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{{#Wiki_filter: | {{#Wiki_filter:WATTS BAR TABLE OF CONTENTS Section Title Page 6.0 ENGINEERED SAFETY FEATURES 6.1 ENGINEERED SAFETY FEATURE MATERIALS 6.1-1 6.1.1 METALLIC MATERIALS 6.1-1 6.1.1.1 MATERIALS SELECTION AND FABRICATION 6.1-1 6.1.1.2 COMPOSITION, COMPATIBILITY, AND STABILITY OF CONTAINMENT AND CORE SPRAY COOLANTS 6.1-2 6.1.2 ORGANIC MATERIALS 6.1-3 6.1.2.1 ELECTRICAL INSULATION 6.1-3 6.1.2.2 SURFACE COATINGS 6.1-3 6.1.2.3 ICE CONDENSER EQUIPMENT 6.1-4 6.1.2.4 IDENTIFICATION TAGS 6.1-4 6.1.2.5 VALVES AND INSTRUMENTS WITHIN CONTAINMENT 6.1-4 6.1.2.6 HEATING AND VENTILATING DOOR SEALS 6.1-5 6.1.2.7 MISCELLANEOUS 6.1-5 6.1.3 POST-ACCIDENT CHEMISTRY 6.1-5 6.1.3.1 BORIC ACID, H3BO3 6.1-5 6.1.3.2 LITHIUM HYDROXIDE 6.1-5 6.1.3.3 SODIUM TETRABORATE 6.1-5 6.1.3.4 FINAL POST-ACCIDENT CHEMISTRY 6.1-6 6.1.4 DEGREE OF COMPLIANCE WITH REGULATORY GUIDE 1.54 FOR PAINTS AND COATINGS INSIDE CONTAINMENT 6.1-6 6.2 CONTAINMENT SYSTEMS 6.2.1 CONTAINMENT FUNCTIONAL DESIGN 6.2.1-1 6.2.1.1 DESIGN BASES 6.2.1-1 6.2.1.1.1 PRIMARY CONTAINMENT DESIGN BASES 6.2.1-1 6.2.1.2 PRIMARY CONTAINMENT SYSTEM DESIGN 6.2.1-3 6.2.1.3 DESIGN EVALUATION 6.2.1-3 6.2.1.3.1 PRIMARY CONTAINMENT EVALUATION 6.2.1-3 6.2.1.3.2 GENERAL DESCRIPTION OF CONTAINMENT PRESSURE ANALYSIS 6.2.1-4 6.2.1.3.3 LONG-TERM CONTAINMENT PRESSURE ANALYSIS 6.2.1-4 6.2.1.3.4 SHORT-TERM BLOWDOWN ANALYSIS 6.2.1-8 Table of Contents 6-i | ||
BLOWDOWN MASS AND ENERGY | |||
MINIMUM SAFETY INJECTION PRINCIPAL PARAMETERS DURING | WATTS BAR TABLE OF CONTENTS Section Title Page 6.2.1.3.5 EFFECT OF STEAM BYPASS 6.2.1-17 6.2.1.3.6 MASS AND ENERGY RELEASE DATA 6.2.1-21 6.2.1.3.7 ACCIDENT CHRONOLOGY 6.2.1-29 6.2.1.3.8 MASS AND ENERGY BALANCE TABLES 6.2.1-29 6.2.1.3.9 CONTAINMENT PRESSURE DIFFERENTIALS 6.2.1-31 6.2.1.3.10 STEAM LINE BREAK INSIDE CONTAINMENT 6.2.1-34 6.2.1.3.11 MAXIMUM REVERSE PRESSURE DIFFERENTIALS 6.2.1-39 6.2.2 CONTAINMENT HEAT REMOVAL SYSTEMS 6.2.2-1 6.2.2.1 DESIGN BASES 6.2.2-1 6.2.2.2 SYSTEM DESIGN 6.2.2-3 6.2.2.3 DESIGN EVALUATION 6.2.2-5 6.2.2.4 TESTING AND INSPECTIONS 6.2.2-7 6.2.2.5 INSTRUMENTATION REQUIREMENTS 6.2.2-8 6.2.2.6 MATERIALS 6.2.2-9 6.2.3 SECONDARY CONTAINMENT FUNCTIONAL DESIGN 6.2.3-1 6.2.3.1 DESIGN BASES 6.2.3-1 6.2.3.1.1 SECONDARY CONTAINMENT ENCLOSURES 6.2.3-1 6.2.3.1.2 EMERGENCY GAS TREATMENT SYSTEM (EGTS) 6.2.3-1 6.2.3.1.3 AUXILIARY BUILDING GAS TREATMENT SYSTEM (ABGTS) 6.2.3-2 6.2.3.2 SYSTEM DESIGN 6.2.3-2 6.2.3.2.1 SECONDARY CONTAINMENT ENCLOSURES 6.2.3-2 6.2.3.2.2 EMERGENCY GAS TREATMENT SYSTEM (EGTS) 6.2.3-6 6.2.3.2.3 AUXILIARY BUILDING GAS TREATMENT SYSTEM (ABGTS) 6.2.3-10 6.2.3.3 DESIGN EVALUATION 6.2.3-12 6.2.3.3.1 SECONDARY CONTAINMENT ENCLOSURES 6.2.3-12 6.2.3.3.2 EMERGENCY GAS TREATMENT SYSTEM (EGTS) 6.2.3-15 6.2.3.3.3 AUXILIARY BUILDING GAS TREATMENT SYSTEM (ABGTS) 6.2.3-19 6.2.3.3.4 TRITIUM PRODUCTION CORE EVALUATION (UNIT 1 ONLY) 6.2.3-22 6.2.3.4 TEST AND INSPECTIONS 6.2.3-22 6.2.3.4.1 EMERGENCY GAS TREATMENT SYSTEM (EGTS) 6.2.3-22 6.2.3.4.2 AUXILIARY BUILDING GAS TREATMENT SYSTEM (ABGTS) 6.2.3-23 6.2.3.5 INSTRUMENTATION REQUIREMENTS 6.2.3-23 6.2.3.5.1 EMERGENCY GAS TREATMENT SYSTEM (EGTS) 6.2.3-23 Table of Contents 6-ii | ||
POST-REFLOOD MASS AND | |||
LOWER | WATTS BAR TABLE OF CONTENTS Section Title Page 6.2.3.5.2 AUXILIARY BUILDING GAS TREATMENT SYSTEM (ABGTS) 6.2.3-24 6.2.4 CONTAINMENT ISOLATION SYSTEMS 6.2.4-1 6.2.4.1 DESIGN BASES 6.2.4-1 6.2.4.2 SYSTEM DESIGN 6.2.4-4 6.2.4.2.1 DESIGN REQUIREMENTS 6.2.4-5 6.2.4.2.2 CONTAINMENT ISOLATION OPERATION 6.2.4-6 6.2.4.2.3 PENETRATION DESIGN 6.2.4-7 6.2.4.3 DESIGN EVALUATION 6.2.4-12 6.2.4.3.1 POSSIBLE LEAKAGE PATHS 6.2.4-15 6.2.4.4 TESTS AND INSPECTIONS 6.2.4-17 6.2.5 COMBUSTIBLE GAS CONTROL IN CONTAINMENT 6.2.5-1 6.2.5.1 DESIGN BASES 6.2.5-1 6.2.5.2 SYSTEM DESIGN 6.2.5-2 6.2.5.3 DESIGN EVALUATION 6.2.5-4 6.2.5.4 TESTING AND INSPECTIONS 6.2.5-5 6.2.5.5 INSTRUMENTATION APPLICATION 6.2.5-5 6.2.6 CONTAINMENT LEAKAGE TESTING 6.2.6-1 6.2.6.1 CONTAINMENT INTEGRATED LEAK RATE TEST 6.2.6-1 6.2.6.2 CONTAINMENT PENETRATION LEAKAGE RATE TEST 6.2.6-2 6.2.6.3 SCHEDULING AND REPORTING OF PERIODIC TESTS 6.2.6-6 6.3 EMERGENCY CORE COOLING SYSTEM 6.3-1 6.3.1 DESIGN BASES 6.3-1 6.3.1.1 RANGE OF COOLANT RUPTURES AND LEAKS 6.3-1 6.3.1.2 FISSION PRODUCT DECAY HEAT 6.3-2 6.3.1.3 REACTIVITY REQUIRED FOR COLD SHUTDOWN 6.3-2 6.3.1.4 CAPABILITY TO MEET FUNCTIONAL REQUIREMENTS 6.3-2 6.3.2 SYSTEM DESIGN 6.3-2 6.3.2.1 SCHEMATIC PIPING AND INSTRUMENTATION DIAGRAMS 6.3-2 6.3.2.2 EQUIPMENT AND COMPONENT DESIGN 6.3-2 6.3.2.3 APPLICABLE CODES AND CLASSIFICATIONS 6.3-16 6.3.2.4 MATERIALS SPECIFICATIONS AND COMPATIBILITY 6.3-16 6.3.2.5 DESIGN PRESSURES AND TEMPERATURES 6.3-16 Table of Contents 6-iii | ||
DEAD-ENDED | |||
List of | WATTS BAR TABLE OF CONTENTS Section Title Page 6.3.2.6 COOLANT QUANTITY 6.3-17 6.3.2.7 PUMP CHARACTERISTICS 6.3-17 6.3.2.8 HEAT EXCHANGER CHARACTERISTICS 6.3-17 6.3.2.9 ECCS FLOW DIAGRAMS 6.3-17 6.3.2.10 RELIEF VALVES 6.3-17 6.3.2.11 SYSTEM RELIABILITY 6.3-17 6.3.2.12 PROTECTION PROVISIONS 6.3-22 6.3.2.13 PROVISIONS FOR PERFORMANCE TESTING 6.3-22 6.3.2.14 NET POSITIVE SUCTION HEAD 6.3-22 6.3.2.15 CONTROL OF MOTOR-OPERATED ISOLATION VALVES 6.3-23 6.3.2.16 MOTOR-OPERATED VALVES AND CONTROLS 6.3-23 6.3.2.17 MANUAL ACTIONS 6.3-23 6.3.2.18 PROCESS INSTRUMENTATION 6.3-23 6.3.2.19 MATERIALS 6.3-24 6.3.3 PERFORMANCE EVALUATION 6.3-24 6.3.3.1 EVALUATION MODEL 6.3-24 6.3.3.2 ECCS PERFORMANCE 6.3-24 6.3.3.3 ALTERNATE ANALYSIS METHODS 6.3-24 6.3.3.4 FUEL ROD PERFORATIONS 6.3-25 6.3.3.5 EFFECTS OF ECCS OPERATION ON THE CORE 6.3-25 6.3.3.6 USE OF DUAL FUNCTION COMPONENTS 6.3-26 6.3.3.7 LAG TIMES 6.3-27 6.3.3.8 THERMAL SHOCK CONSIDERATIONS 6.3-28 6.3.3.9 LIMITS ON SYSTEM PARAMETERS 6.3-28 6.3.3.10 USE OF RHR SPRAY 6.3-28 6.3.4 TESTS AND INSPECTIONS 6.3-29 6.3.4.1 PREOPERATIONAL TESTS 6.3-29 6.3.4.2 COMPONENT TESTING 6.3-29 6.3.4.3 PERIODIC SYSTEM TESTING 6.3-30 6.3.5 INSTRUMENTATION APPLICATION 6.3-30 6.3.5.1 TEMPERATURE INDICATION 6.3-30 6.3.5.2 PRESSURE INDICATION 6.3-30 6.3.5.3 FLOW INDICATION 6.3-31 6.3.5.4 LEVEL INDICATION 6.3-31 Table of Contents 6-iv | ||
List of | |||
AIR LEAKAGE (EXFILTRATION) | WATTS BAR TABLE OF CONTENTS Section Title Page 6.3.5.5 VALVE POSITION INDICATION 6.3-32 6.4 HABITABILITY SYSTEMS 6.4-1 6.4.1 DESIGN BASES 6.4-1 6.4.2 SYSTEM DESIGN 6.4-1 6.4.2.1 DEFINITION OF MCRHS AREA 6.4-1 6.4.2.2 VENTILATION SYSTEM DESIGN 6.4-2 6.4.2.3 LEAK TIGHTNESS 6.4-2 6.4.2.4 INTERACTION WITH OTHER ZONES AND PRESSURE-CONTAINING EQUIPMENT 6.4-3 6.4.2.5 SHIELDING DESIGN 6.4-4 6.4.2.6 CONTROL ROOM EMERGENCY PROVISIONS 6.4-4 6.4.2.7 MCRHS FIRE PROTECTION 6.4-4 6.4.3 SYSTEM OPERATIONAL PROCEDURES 6.4-5 6.4.4 DESIGN EVALUATIONS 6.4-7 6.4.4.1 RADIOLOGICAL PROTECTION 6.4-7 6.4.4.2 TOXIC GAS PROTECTION 6.4-7 6.4.5 TESTING AND INSPECTION 6.4-9 6.4.6 INSTRUMENTATION REQUIREMENTS 6.4-9 6.5 FISSION PRODUCT REMOVAL AND CONTROL SYSTEMS 6.5-1 6.5.1 ENGINEERED SAFETY FEATURE (ESF) FILTER SYSTEMS 6.5-1 6.5.1.1 DESIGN BASES 6.5-1 6.5.1.2 SYSTEM DESIGN 6.5-2 6.5.1.3 DESIGN EVALUATION 6.5-4 6.5.1.4 TESTS AND INSPECTIONS 6.5-5 6.5.1.5 INSTRUMENTATION REQUIREMENTS 6.5-5 6.5.1.6 MATERIALS 6.5-6 6.5.2 CONTAINMENT SPRAY SYSTEM FOR FISSION PRODUCT CLEANUP 6.5-7 6.5.2.1 DESIGN BASES 6.5-7 6.5.2.2 SYSTEM DESIGN 6.5-7 6.5.2.3 DESIGN EVALUATION 6.5-7 6.5.2.4 TESTS AND INSPECTIONS 6.5-7 6.5.2.5 INSTRUMENTATION REQUIREMENTS 6.5-7 6.5.2.6 MATERIALS 6.5-7 Table of Contents 6-v | ||
PATHS IN THE WATTS BAR MCRHS AREA CONTROL | |||
PATHS IN THE WATTS BAR MCRHS AREA CONTROL | WATTS BAR TABLE OF CONTENTS Section Title Page 6.5.3 FISSION PRODUCT CONTROL SYSTEMS 6.5-7 6.5.3.1 PRIMARY CONTAINMENT 6.5-7 6.5.3.2 SECONDARY CONTAINMENTS 6.5-9 6.5.4 ICE CONDENSER AS A FISSION PRODUCT CLEANUP SYSTEM 6.5-10 6.5.4.1 ICE CONDENSER DESIGN BASIS (FISSION PRODUCT CLEANUP FUNCTION) 6.5-10 6.5.4.2 ICE CONDENSER SYSTEM DESIGN 6.5-10 6.5.4.3 ICE CONDENSER SYSTEM DESIGN EVALUATION (FISSION PRODUCT CLEANUP FUNCTION) 6.5-11 6.5.4.4 CONDENSER SYSTEM TESTS AND INSPECTIONS 6.5-13 6.5.4.5 ICE CONDENSER MATERIALS 6.5-13 6.6 INSERVICE INSPECTION OF ASME CODE CLASS 2 AND 3 COMPONENTS 6.6-1 6.6.1 COMPONENTS SUBJECT TO EXAMINATION AND/OR TEST 6.6-1 6.6.2 ACCESSIBILITY 6.6-1 6.6.3 EXAMINATION TECHNIQUES AND PROCEDURES 6.6-1 6.6.4 INSPECTION INTERVALS 6.6-1 6.6.5 EXAMINATION CATEGORIES AND REQUIREMENTS 6.6-1 6.6.6 EVALUATION OF EXAMINATION RESULTS 6.6-1 6.6.7 SYSTEM PRESSURE TESTS 6.6-2 6.6.8 PROTECTION AGAINST POSTULATED PIPING FAILURES 6.6-2 6.7 ICE CONDENSER SYSTEM 6.7-1 6.7.1 FLOOR STRUCTURE AND COOLING SYSTEM 6.7-1 6.7.1.1 DESIGN BASES 6.7-1 6.7.1.2 SYSTEM DESIGN 6.7-4 6.7.1.3 DESIGN EVALUATION 6.7-5 6.7.2 WALL PANELS 6.7-8 6.7.2.1 DESIGN BASIS 6.7-8 6.7.2.2 SYSTEM DESIGN 6.7-8 6.7.2.3 DESIGN EVALUATION 6.7-9 6.7.3 LATTICE FRAMES AND SUPPORT COLUMNS 6.7-9 6.7.3.1 DESIGN BASIS 6.7-9 6.7.3.2 SYSTEM DESIGN 6.7-12 6.7.3.3 DESIGN EVALUATION 6.7-13 Table of Contents 6-vi | ||
WATTS BAR TABLE OF CONTENTS Section Title Page 6.7.4 ICE BASKETS 6.7-14 6.7.4.1 DESIGN BASIS 6.7-14 6.7.4.2 SYSTEM DESIGN 6.7-16 6.7.4.3 DESIGN EVALUATION 6.7-18 6.7.5 CRANE AND RAIL ASSEMBLY 6.7-20 6.7.5.1 DESIGN BASIS 6.7-20 6.7.5.2 SYSTEM DESIGN 6.7-21 6.7.5.3 DESIGN EVALUATION 6.7-21 6.7.6 REFRIGERATION SYSTEM 6.7-22 6.7.6.1 DESIGN BASIS 6.7-22 6.7.6.2 SYSTEM DESIGN 6.7-23 6.7.6.3 DESIGN EVALUATION 6.7-26 6.7.7 AIR HANDLING UNITS 6.7-30 6.7.7.1 DESIGN BASIS 6.7-30 6.7.7.2 SYSTEM DESIGN 6.7-31 6.7.7.3 DESIGN EVALUATION 6.7-31 6.7.8 LOWER INLET DOORS 6.7-32 6.7.8.1 DESIGN BASIS 6.7-32 6.7.8.2 SYSTEM DESIGN 6.7-35 6.7.8.3 DESIGN EVALUATION 6.7-37 6.7.9 LOWER SUPPORT STRUCTURE 6.7-38 6.7.9.1 DESIGN BASIS 6.7-38 6.7.9.2 SYSTEM DESIGN 6.7-39 6.7.9.3 DESIGN EVALUATION 6.7-41 6.7.10 TOP DECK AND DOORS 6.7-50 6.7.10.1 DESIGN BASIS 6.7-50 6.7.10.2 SYSTEM DESIGN 6.7-51 6.7.11 INTERMEDIATE DECK AND DOORS 6.7-55 6.7.11.1 DESIGN BASIS 6.7-55 6.7.11.2 SYSTEM DESIGN 6.7-56 6.7.11.3 DESIGN EVALUATION 6.7-57 6.7.12 AIR DISTRIBUTION DUCTS 6.7-58 6.7.12.1 DESIGN BASIS 6.7-58 6.7.12.2 SYSTEM DESIGN 6.7-59 Table of Contents 6-vii | |||
WATTS BAR TABLE OF CONTENTS Section Title Page 6.7.12.3 DESIGN EVALUATION 6.7-59 6.7.13 EQUIPMENT ACCESS DOOR 6.7-59 6.7.13.1 DESIGN BASIS 6.7-59 6.7.13.2 SYSTEM DESIGN 6.7-60 6.7.13.3 DESIGN EVALUATION 6.7-60 6.7.14 ICE TECHNOLOGY, ICE PERFORMANCE, AND ICE CHEMISTRY 6.7-60 6.7.14.1 DESIGN BASIS 6.7-60 6.7.14.2 SYSTEM DESIGN 6.7-61 6.7.14.3 DESIGN EVALUATION 6.7-61 6.7.15 ICE CONDENSER INSTRUMENTATION 6.7-66 6.7.15.1 DESIGN BASIS 6.7-66 6.7.15.2 DESIGN DESCRIPTION 6.7-67 6.7.15.3 DESIGN EVALUATION 6.7-69 6.7.16 ICE CONDENSER STRUCTURAL DESIGN 6.7-69 6.7.16.1 APPLICABLE CODES, STANDARDS, AND SPECIFICATIONS 6.7-69 6.7.16.2 LOADS AND LOADING COMBINATIONS 6.7-69 6.7.16.3 DESIGN AND ANALYTICAL PROCEDURES 6.7-70 6.7.16.4 STRUCTURAL ACCEPTANCE CRITERIA 6.7-71 6.7.17 SEISMIC ANALYSIS 6.7-72 6.7.17.1 SEISMIC ANALYSIS METHODS 6.7-72 6.7.17.2 SEISMIC LOAD DEVELOPMENT 6.7-74 6.7.17.3 VERTICAL SEISMIC RESPONSE 6.7-76 6.7.18 MATERIALS 6.7-76 6.7.18.1 DESIGN CRITERIA 6.7-76 6.7.18.2 ENVIRONMENTAL EFFECTS 6.7-77 6.7.18.3 COMPLIANCE WITH 10 CFR 50, APPENDIX B 6.7-78 6.7.18.4 MATERIALS SPECIFICATIONS 6.7-79 6.7.19 TESTS AND INSPECTIONS 6.7-80 6.8 AIR RETURN FANS 6.8-1 6.8.1 DESIGN BASES 6.8-1 6.8.2 SYSTEM DESCRIPTION 6.8-1 6.8.3 SAFETY EVALUATION 6.8-2 6.8.4 INSPECTION AND TESTING 6.8-3 6.8.5 INSTRUMENTATION REQUIREMENTS 6.8-3 Table of Contents 6-viii | |||
WATTS BAR TABLE OF CONTENTS Section Title Page 6.9 MOTOR-OPERATED VALVE (MOV) PROGRAMS6.9-1 Table of Contents 6-ix | |||
WATTS BAR TABLE OF CONTENTS Section Title Page THIS PAGE INTENTIONALLY BLANK Table of Contents 6-x | |||
WATTS BAR LIST OF TABLES Section Title TABLE 6.1-1 DELETED BY AMENDMENT 97 TABLE 6.2.1-1 STRUCTURAL HEAT SINKS TABLE 6.2.1-2 PUMP FLOW RATES VS. TIME TABLE 6.2.1-3 ENERGY BALANCES TABLE 6.2.1-4 ENERGY BALANCES TABLE 6.2.1-5 MATERIAL PROPERTY DATA TABLE 6.2.1-6 TMD INPUT FOR WATTS BAR TABLE 6.2.1-7 TMD FLOW INPUT DATA FOR WATTS BAR TABLE 6.2.1-8 CALCULATED MAXIMUM PEAK PRESSURES IN LOWER COMPARTMENT ELEMENTS ASSUMING UNAUGMENTED FLOW TABLE 6.2.1-9 CALCULATED MAXIMUM PEAK PRESSURES IN THE ICE CONDENSER COMPARTMENT ASSUMING UNAUGMENTED FLOW TABLE 6.2.1-10 CALCULATED MAXIMUM DIFFERENTIAL PRESSURES ACROSS THE OPERATING DECK OR LOWER CRANE WALL ASSUMING UNAUGMENTED FLOW TABLE 6.2.1-11 CALCULATED MAXIMUM DIFFERENTIAL PRESSURES ACROSS THE UPPER CRANE WALL ASSUMING UNAUGMENTED FLOW TABLE 6.2.1-12 SENSITIVITY STUDIES FOR D. C. COOK PLANT TABLE 6.2.1-13 WATTS BAR ICE CONDENSER DESIGN PARAMETERS TABLE 6.2.1-14 ALLOWABLE LEAKAGE AREA FOR VARIOUS REACTOR COOLANT SYSTEM BREAK SIZES TABLE 6.2.1-15 SYSTEM PARAMETERS INITIAL CONDITIONS TABLE 6.2.1-16 DOUBLE-ENDED PUMP SUCTION GUILLOTINE BREAK - | |||
BLOWDOWN MASS AND ENERGY RELEASES TABLE 6.2.1-17 DOUBLE-ENDED PUMP SUCTION GUILLOTINE BREAK - | |||
REFLOOD MASS AND ENERGY RELEASE - MINIMUM SAFETY INJECTION TABLE 6.2.1-18 DOUBLE-ENDED PUMP SUCTION GUILLOTINE BREAK - | |||
MINIMUM SAFETY INJECTION PRINCIPAL PARAMETERS DURING REFLOOD TABLE 6.2.1-19 DOUBLE-ENDED PUMP SUCTION GUILLOTINE BREAK - | |||
POST-REFLOOD MASS AND ENERGY RELEASES - MINIMUM SAFETY INJECTION TABLE 6.2.1-20 DECAY HEAT CURVE List of Tables 6-xi | |||
WATTS BAR LIST OF TABLES Section Title TABLE 6.2.1-21 DELETED BY AMENDMENT 97 TABLE 6.2.1-22 DELETED BY AMENDMENT 97 TABLE 6.2.1-23 BREAK MASS AND ENERGY FLOW FROM A DOUBLE-ENDED COLD LEG GUILLOTINE BREAK TABLE 6.2.1-24 BREAK MASS AND ENERGY FLOW FROM A DOUBLE-ENDED HOT LEG GUILLOTINE BREAK TABLE 6.2.1-25 DOUBLE-ENDED PUMP SUCTION LOCA SEQUENCE OF EVENTS TABLE 6.2.1-26A DOUBLE-ENDED PUMP SUCTION GUILLOTINE BREAK MINIMUM SAFETY INJECTION - MASS BALANCE TABLE 6.2.1-26B DOUBLE-ENDED PUMP SUCTION GUILLOTINE BREAK MINIMUM SAFETY INJECTION - ENERGY BALANCE TABLE 6.2.1-27A STEAM LINE BREAK BLOWDOWN TABLE 6.2.1-27B STEAM GENERATOR ENCLOSURE GEOMETRY TABLE 6.2.1-27C STEAM GENERATOR ENCLOSURE FLOW PATH DATA TABLE 6.2.1-27D PEAK DIFFERENTIAL PRESSURE - STEAM GENERATOR ENCLOSURE TABLE 6.2.1-28 MASS AND ENERGY RELEASE RATES INTO PRESSURIZER ENCLOSURE TABLE 6.2.1-29A PRESSURIZER GEOMETRIC DATA TABLE 6.2.1-29B PEAK DIFFERENTIAL PRESSURE - PRESSURIZER ENCLOSURE TABLE 6.2.1-30 MASS AND ENERGY RELEASE RATES 127 IN2 COLD LEG TABLE 6.2.1-31 REACTOR CAVITY VOLUMES TABLE 6.2.1-32 FLOW PATH DATA (REACTOR CAVITY) | |||
TABLE 6.2.1-33 CONTAINMENT DATA (ECCS ANALYSIS) | |||
TABLE 6.2.1-34 MAJOR CHARACTERISTICS OF STRUCTURAL HEAT SINKS INSIDE SEQUOYAH NUCLEAR PLANT CONTAINMENT - | |||
UPPER COMPARTMENT TABLE 6.2.1-35 MAJOR CHARACTERISTICS OF STRUCTURAL HEAT SINKS INSIDE SEQUOYAH NUCLEAR PLANT CONTAINMENT - | |||
LOWER COMPARTMENT TABLE 6.2.1-36 MAJOR CHARACTERISTICS OF STRUCTURAL HEAT SINKS INSIDE SEQUOYAH NUCLEAR PLANT CONTAINMENT - | |||
DEAD-ENDED COMPARTMENT TABLE 6.2.1-37 MAXIMUM REVERSE PRESSURE DIFFERENTIAL PRESSURE ANALYSIS BASE CASE List of Tables 6-xii | |||
WATTS BAR LIST OF TABLES Section Title TABLE 6.2.1-38 ICE CONDENSER STEAM EXIT FLOW VS. TIME VS. SUMP TEMPERATURE TABLE 6.2.1-39 MASS AND ENERGY RELEASE RATES FOR SPECIFIED STEAM LINE BREAKS TABLE 6.2.1-39 MASS AND ENERGY RELEASE RATES FOR SPECIFIED STEAM LINE BREAKS (CONTD) | |||
TABLE 6.2.1-39 MASS AND ENERGY RELEASE RATES FOR SPECIFIED STEAM LINE BREAKS (CONTD) | |||
TABLE 6.2.1-40 STEAM LINE BREAK CASES FOR CORE INTEGRITY TABLE 6.2.1-41 LINE BREAK(1) DESCRIPTIONS FOR MASS AND ENERGY RELEASES TABLE 6.2.1-42 SMALL BREAK DESCRIPTIONS FOR MASS AND ENERGY TABLE 6.2.1-43 LARGE BREAK ANALYSIS - ASSOCIATED TIMES TABLE 6.2.1-44 SMALL BREAK ANALYSIS - SMALL SPLIT - ASSOCIATED TIMES TABLE 6.2.1-45 SAFETY INJECTION FLOW MINIMUM SAFEGUARDS TABLE 6.2.2-1 CONTAINMENT SPRAY PUMP/MOTOR DESIGN PARAMETERS TABLE 6.2.2-2 CONTAINMENT SPRAY HEAT EXCHANGER DESIGN PARAMETERS TABLE 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS TABLE 6.2.3-1 DUAL CONTAINMENT CHARACTERISTICS TABLE 6.2.3-2 FAILURE MODES AND EFFECTS ANALYSIS EMERGENCY GAS TREATMENT SYSTEM TABLE 6.2.3-3 FAILURE MODES AND EFFECTS ANALYSIS FOR PASSIVE FAILURE FOR THE ABGTS TABLE 6.2.3-3 FAILURE MODES AND EFFECTS ANALYSIS FOR THE ABGTS TABLE 6.2.4-1 WATTS BAR NUCLEAR PLANT CONTAINMENT PENETRATIONS AND BARRIERS TABLE 6.2.4-1 WATTS BAR NUCLEAR PLANT CONTAINMENT PENETRATIONS AND BARRIERS (SHEET 65 OF 69) | |||
TABLE 6.2.4-1 WATTS BAR NUCLEAR PLANT CONTAINMENT PENETRATIONS AND BARRIERS (SHEET 66 OF 69) | |||
TABLE 6.2.4-1 WATTS BAR NUCLEAR PLANT CONTAINMENT PENETRATIONS AND BARRIERS (SHEET 67 OF 69) | |||
List of Tables 6-xiii | |||
WATTS BAR LIST OF TABLES Section Title TABLE 6.2.4-1 WATTS BAR NUCLEAR PLANT CONTAINMENT PENETRATIONS AND BARRIERS (SHEET 68 OF 69) | |||
TABLE 6.2.4-1 WATTS BAR NUCLEAR PLANT CONTAINMENT PENETRATIONS AND BARRIERS (SHEET 69 OF 69) | |||
TABLE 6.2.4-2 POSSIBLE BYPASS LEAKAGE PATHS TO THE AUXILIARY BUILDING TABLE 6.2.4-3 PREVENTION OF BYPASS LEAKAGE TO THE ATMOSPHERE TABLE 6.2.4-4 INSTRUMENT LINES PENETRATING PRIMARY CONTAINMENT TABLE 6.2.6-1 PENETRATIONS SUBJECTED TO TYPE B TESTING TABLE 6.2.6-2 CONTAINMENT ISOLATION VALVES SUBJECTED TO TYPE C TESTING TABLE 6.2.6-3 VALVES EXEMPTED FROM TYPE C LEAK TESTING TABLE 6.2.6-4 CONTAINMENT VESSEL PRESSURE AND LEAK TEST REACTOR BUILDING CONTAINMENT PENETRATION STATUS TABLE 6.3-1 EMERGENCY CORE COOLING SYSTEM COMPONENT PARAMETERS TABLE 6.3-2 MATERIALS EMPLOYED FOR EMERGENCY CORE COOLING SYSTEM COMPONENTS TABLE 6.3-3 SEQUENCE OF CHANGE-OVER OPERATION, INJECTION TO RECIRCULATION TABLE 6.3-3A EVALUATION OF TIME SEQUENCE ASSOCIATED WITH CHANGEOVER OPERATION FROM INJECTION TO RECIRCULATION TABLE 6.3-4 NORMAL OPERATING STATUS OF EMERGENCY CORE COOLING SYSTEM COMPONENTS FOR CORE COOLING TABLE 6.3-5 EMERGENCY CORE COOLING SYSTEM SHARED FUNCTIONS EVALUATION TABLE 6.3-6 MAXIMUM RECIRCULATION LOOP LEAKAGE EXTERNAL TO CONTAINMENT TABLE 6.3-7 DELETED BY AMENDMENT 85 TABLE 6.3-8 FAILURE MODES AND EFFECTS ANALYSIS FOR ACTIVE FAILURES FOR THE SAFETY INJECTION SYSTEM TABLE 6.3-9 FAILURE MODES AND EFFECTS ANALYSIS FOR THE SAFETY INJECTION SYSTEM (PASSIVE FAILURES RECIRC. MODE) | |||
List of Tables 6-xiv | |||
WATTS BAR LIST OF TABLES Section Title TABLE 6.3-10 PRINCIPAL ECCS VALVE POSITIONS TABLE 6.3-11 NORMALIZED DECAY HEAT TABLE 6.3-12 AVAILABLE NPSH DURING ECCS OPERATION TABLE 6.4-1 (SHEET 1 OF 1) | |||
AIR LEAKAGE (EXFILTRATION) PATHS IN THE WATTS BAR MCRHS AREA CONTROL ROOM TABLE 6.4-2 (SHEET 1 OF 1) | |||
AIR LEAKAGE (INFILTRATION) PATHS IN THE WATTS BAR MCRHS AREA CONTROL ROOM TABLE 6.5-1 REGULATORY GUIDE 1.52, REV. 2, SECTION APPLICABILITY FOR THE EMERGENCY GAS TREATMENT SYSTEM TABLE 6.5-2 REGULATORY GUIDE 1.52, REV. 2, SECTION APPLICABILITY FOR THE AUXILIARY BUILDING GAS TREATMENT SYSTEM TABLE 6.5-3 DELETED BY AMENDMENT 111 TABLE 6.5-4 REGULATORY GUIDE 1.52, REV. 2, SECTION APPLICABILITY FOR THE MAIN CONTROL ROOM AIR CLEANUP SUBSYSTEM TABLE 6.5-5 ESF AIR CLEANUP UNIT DATA TABLE 6.5-6 DELETED IN FSAR AMENDMENT 65 TABLE 6.5-7 PRIMARY CONTAINMENT OPERATION FOLLOWING A DBA TABLE 6.5-8 SECONDARY CONTAINMENT OPERATION FOLLOWING A DBA TABLE 6.7-1 WALL PANEL DESIGN LOADS(1) | |||
TABLE 6.7-2 ICE BASKET LOAD | |||
==SUMMARY== | ==SUMMARY== | ||
MINIMUM TEST | MINIMUM TEST LOADS TABLE 6.7-3 | ||
==SUMMARY== | ==SUMMARY== | ||
OF STRESSES IN BASKET DUE TO DESIGN | OF STRESSES IN BASKET DUE TO DESIGN LOADS TABLE 6.7-4 ICE BASKET MATERIAL MINIMUM YIELD STRESS TABLE 6.7-5 ALLOWABLE STRESS LIMITS (D + OBE) FOR ICE BASKET MATERIALS TABLE 6.7-6 ALLOWABLE STRESS LIMITS (D + SSE), (D + DBA) FOR ICE BASKET MATERIALS TABLE 6.7-7 ALLOWABLE STRESS LIMITS (D + SSE + DBA) FOR ICE BASKET MATERIALS TABLE 6.7-8 ICE BASKET CLEVIS PIN STRESS | ||
==SUMMARY== | ==SUMMARY== | ||
TABLE 6.7- | |||
TABLE 6.7-9 ICE BASKET MOUNTING BRACKET ASSEMBLY STRESS | |||
==SUMMARY== | ==SUMMARY== | ||
TABLE 6.7- | |||
TABLE 6.7-10 ICE BASKET PLATE STRESS | |||
==SUMMARY== | ==SUMMARY== | ||
TABLE 6.7- | |||
TABLE 6.7-11 ICE BASKET V-BOLT STRESS | |||
==SUMMARY== | ==SUMMARY== | ||
List of | List of Tables 6-xv | ||
WATTS BAR LIST OF TABLES Section Title TABLE 6.7-12 ICE BASKET - BASKET END STRESS | |||
==SUMMARY== | ==SUMMARY== | ||
TABLE 6.7- | |||
TABLE 6.7-13 ICE BUCKET COUPLING SCREW STRESS | |||
==SUMMARY== | ==SUMMARY== | ||
3 INCH ELEVATION(1)TABLE 6.7- | 3 INCH ELEVATION(1) | ||
TABLE 6.7-14 ICE BUCKET COUPLING SCREW STRESS | |||
==SUMMARY== | ==SUMMARY== | ||
12 FOOT ELEVATION(1)TABLE 6.7- | 12 FOOT ELEVATION(1) | ||
TABLE 6.7-15 ICE BASKET COUPLING SCREW STRESS | |||
==SUMMARY== | ==SUMMARY== | ||
24 FOOT ELEVATION(1)TABLE 6.7- | 24 FOOT ELEVATION(1) | ||
TABLE 6.7-16 ICE BUCKET COUPLING SCREW STRESS | |||
==SUMMARY== | ==SUMMARY== | ||
36 FOOT ELEVATION(1)TABLE 6.7- | 36 FOOT ELEVATION(1) | ||
TABLE 6.7-17 CRANE AND RAIL ASSEMBLY DESIGN LOADS TABLE 6.7-18 REFRIGERATION SYSTEM PARAMETERS TABLE 6.7-18 REFRIGERATION SYSTEM PARAMETERS CONTINUED TABLE 6.7-19 LOWER INLET DOOR DESIGN PARAMETERS AND LOADS TABLE 6.7-20 DESIGN LOADS AND PARAMETERS TOP DECK TABLE 6.7-21 | |||
==SUMMARY== | ==SUMMARY== | ||
OF RESULTS UPPER BLANKET DOOR STRUCTURAL ANALYSIS - | OF RESULTS UPPER BLANKET DOOR STRUCTURAL ANALYSIS - LOCA TABLE 6.7-22 DESIGN LOADS AND PARAMETERS INTERMEDIATE DECK TABLE 6.7-23 | ||
==SUMMARY== | ==SUMMARY== | ||
OF WALTZ MILL TESTS TABLE 6.7- | OF WALTZ MILL TESTS TABLE 6.7-24 ICE CONDENSER RTDS TABLE 6.7-25 ICE CONDENSER ALLOWABLE LIMITS (1) | ||
TABLE 6.7-26 SELECTION OF STRUCTURAL STEELS IN RELATION TO PREVENTION OF NON-DUCTILE FRACTURE OF ICE CONDENSER COMPONENTS TABLE 6.7-27 | |||
==SUMMARY== | ==SUMMARY== | ||
OF WATTS BAR LOADS - TANGENTIAL CASE OBTAINED USING THE TWO-MASS DYNAMIC | OF WATTS BAR LOADS - TANGENTIAL CASE OBTAINED USING THE TWO-MASS DYNAMIC MODEL TABLE 6.7-28 | ||
==SUMMARY== | ==SUMMARY== | ||
OF WATTS BAR LOADS - RADIAL CASE OBTAINED USING THE TWO-MASS DYNAMIC | OF WATTS BAR LOADS - RADIAL CASE OBTAINED USING THE TWO-MASS DYNAMIC MODEL TABLE 6.7-29 | ||
==SUMMARY== | ==SUMMARY== | ||
OF LOAD | OF LOAD RESULTS OF FIVE NON-LINEAR DYNAMIC MODELS TABLE 6.7-30 | ||
==SUMMARY== | ==SUMMARY== | ||
OF | OF PARAMETERS USED IN THE SEISMIC ANALYSIS List of Tables 6-xvi | ||
List of | |||
List of | WATTS BAR LIST OF FIGURES Section Title FIGURE 6.1-1 DELETED BY AMENDMENT 97 FIGURE 6.2.1-1 CONTAINMENT PRESSURE VERSUS TIME FIGURE 6.2.1-2A UPPER COMPARTMENT TEMPERATURE VERSUS TIME FIGURE 6.2.1-2B LOWER COMPARTMENT TEMPERATURE VERSUS TIME FIGURE 6.2.1-3 ACTIVE AND INACTIVE SUMP TEMPERATURE TRANSIENTS FIGURE 6.2.1-4 MELTED ICE MASS TRANSIENT FIGURE 6.2.1-4A COMPARISON OF CONTAINMENT PRESSURE VERSUS ICE MELT FIGURE 6.2.1-5 PLAN AT EQUIPMENT ROOMS ELEVATION FIGURE 6.2.1-6 CONTAINMENT SECTION VIEW FIGURE 6.2.1-7 PLAN VIEW AT ICE CONDENSER ELEVATION ICE CONDENSER COMPARTMENTS FIGURE 6.2.1-8 LAYOUT OF CONTAINMENT SHELL FIGURE 6.2.1-9 TMD CODE NETWORK FIGURE 6.2.1-10 UPPER AND LOWER COMPARTMENT PRESSURE TRANSIENT FOR WORST CASE BREAK COMPARTMENT (ELEMENT 1) HAVING A DEHL BREAK FIGURE 6.2.1-11 UPPER AND LOWER COMPARTMENT PRESSURE TRANSIENT FOR WORST CASE BREAK COMPARTMENT (ELEMENT 1) HAVING A DECL BREAK. | ||
& 2 ELECTRICAL LOGIC DIAGRAM - | FIGURE 6.2.1-12 ILLUSTRATION OF CHOKED FLOW CHARACTERISTICS FIGURE 6.2.1-13 SENSITIVITY OF PEAK PRESSURE TO AIR COMPRESSION RATIO FIGURE 6.2.1-14 STEAM CONCENTRATION IN A VERTICAL DISTRIBUTION CHANNEL FIGURE 6.2.1-15 PEAK COMPRESSION PRESSURE VERSUS COMPRESSION RATIO FIGURE 6.2.1-16 PEAK COMPARTMENT PRESSURE VERSUS BLOWDOWN RATE FIGURE 6.2.1-17 SENSITIVITY OF PEAK COMPRESSION PRESSURE TO DECK BYPASS FIGURE 6.2.1-18 PRESSURE INCREASE VERSUS DECK AREA FROM DECK LEAKAGE TESTS FIGURE 6.2.1-19 ENERGY RELEASE AT TIME OF COMPRESSION PEAK PRESSURE FROM List of Figures 6-xvii | ||
EMERGENCY GAS TREATMENT | |||
& 2 ELECTRICAL LOGIC DIAGRAM - | WATTS BAR LIST OF FIGURES Section Title FULL-SCALE SECTION TESTS WITH 1-FOOT DIAMETER BASKETS FIGURE 6.2.1-20 PRESSURE INCREASE VERSUS DECK AREA FROM DECK LEAKAGE TESTS FIGURE 6.2.1-21 DELETED BY AMENDMENT 97 FIGURE 6.2.1-22 DELETED BY AMENDMENT 97 FIGURE 6.2.1-23 DELETED BY AMENDMENT 97 FIGURE 6.2.1-24 DELETED BY AMENDMENT 97 FIGURE 6.2.1-25 DELETED BY AMENDMENT 97 FIGURE 6.2.1-26 DELETED BY AMENDMENT 97 FIGURE 6.2.1-27 CONTAINMENT MODEL SCHEMATIC. | ||
EMERGENCY GAS | FIGURE 6.2.1-28 REACTOR CAVITY TMD NETWORK. | ||
EMERGENCY GAS | FIGURE 6.2.1-29 REACTOR VESSEL ANNULUS FIGURE 6.2.1-30 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | ||
EMERGENCY GAS | FIGURE 6.2.1-31 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | ||
FIGURE 6.2.1-32 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-33 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-34 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-35 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-36 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-37 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-38 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-39 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-40 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
List of Figures 6-xviii | |||
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.2.1-41 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-42 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-43 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-44 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-45 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-46 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-47 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-48 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-49 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-50 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-51 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-52 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-53 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-54 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-55 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-56 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-57 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-58 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-59 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
List of Figures 6-xix | |||
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.2.1-60 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-61 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-62 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-63 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-64 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-65 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-66 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-67 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-68 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS) | |||
FIGURE 6.2.1-69 COMPARTMENT TEMPERATURE 1.4 FT2/LOOP, 100.6% POWER AFW RUNOUT PROTECTION FAILURE FIGURE 6.2.1-70 LOWER COMPARTMENT PRESSURE 1.4 FT2 LOOP, 100.6% | |||
POWER AFW RUNOUT PROTECTION FAILURE FIGURE 6.2.1-71 COMPARTMENT TEMPERATURE 0.35 FT2 SPLIT, 30% POWER AFW RUNOUT PROTECTION FAILURE FIGURE 6.2.1-72 LOWER COMPARTMENT PRESSURE 0.35 FT2 SPLIT, 30% | |||
POWER AFW RUNOUT PROTECTION FAILURE FIGURE 6.2.1-73 COMPARTMENT TEMPERATURE 0.6 FT2 SPLIT, 30% POWER AFW RUNOUT PROTECTION FAILURE FIGURE 6.2.1-74 LOWER COMPARTMENT PRESSURE 0.6 FT2 SPLIT, 30% | |||
POWER AFW RUNOUT PROTECTION FAILURE FIGURE 6.2.1-75 MAXIMUM REVERSE PRESSURE DIFFERENTIAL MODEL FIGURE 6.2.1-76 MAXIMUM REVERSE PRESSURE DIFFERENTIAL UPPER AND LOWER COMPARTMENT PRESSURES FIGURE 6.2.1-77 MAXIMUM REVERSE PRESSURE DIFFERENTIAL UPPER AND LOWER COMPARTMENT TEMPERATURES FIGURE 6.2.1-78 MAXIMUM REVERSE PRESSURE DIFFERENTIAL UPPER TO LOWER COMPARTMENT FLOWRATES List of Figures 6-xx | |||
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.2.1-79 MAXIMUM REVERSE PRESSURE DIFFERENTIAL CASE 6 UPPER AND LOWER COMPARTMENT PRESSURES FIGURE 6.2.1-80 MAXIMUM REVERSE PRESSURE DIFFERENTIAL CASE 6 UPPER AND LOWER COMPARTMENT TEMPERATURES FIGURE 6.2.1-81 STEAM GENERATOR ENCLOSURE NODALIZATION FIGURE 6.2.1-82 FLOW PATHS FOR TMD STEAM GENERATOR ENCLOSURE SHORT-TERM PRESSURE ANALYSIS FIGURE 6.2.1-83 PRESSURE TRANSIENT BETWEEN BREAK ELEMENT AND UPPER COMPARTMENT (STEAM GENERATOR ENCLOSURE ANALYSIS) | |||
FIGURE 6.2.1-84 DIFFERENTIAL PRESSURE TRANSIENT ACROSS THE STEAM GENERATOR VESSEL (STEAM GENERATOR ENCLOSURE ANALYSIS) | |||
FIGURE 6.2.1-85 DIFFERENTIAL PRESSURE TRANSIENT ACROSS THE STEAM GENERATOR VESSEL (STEAM GENERATOR ENCLOSURE ANALYSIS) | |||
FIGURE 6.2.1-86 PRESSURE VERSUS TIME FOR THE BREAK ELEMENT (STEAM GENERATOR ENCLOSURE ANALYSIS) | |||
FIGURE 6.2.1-86A UPPER COMPARTMENT PRESSURE VERSUS TIME (STEAM GENERATOR ENCLOSURE ANALYSIS) | |||
FIGURE 6.2.1-87 NODALIZATION PRESSURE ENCLOSURE ANALYSIS FIGURE 6.2.1-88 PRESSURE TRANSIENT BETWEEN BREAK ELEMENT AND UPPER COMPARTMENT (PRESSURIZER ENCLOSURE ANALYSIS) | |||
FIGURE 6.2.1-89 PRESSURE DIFFERENTIAL ACROSS THE PRESSURIZER VESSEL (PRESSURIZER ENCLOSURE ANALYSIS) | |||
FIGURE 6.2.1-90 PRESSURE DIFFERENTIAL ACROSS THE PRESSURIZER VESSEL (PRESSURIZER ENCLOSURE ANALYSIS) | |||
FIGURE 6.2.1-91 PRESSURE DIFFERENTIAL ACROSS THE PRESSURIZER VESSEL (PRESSURIZER ENCLOSURE ANALYSIS) | |||
FIGURE 6.2.1-92 PRESSURE VERSUS TIME FOR THE BREAK ELEMENT (PRESSURIZER ENCLOSURE ANALYSIS) | |||
FIGURE 6.2.2-1 POWERHOUSE UNITS 1 & 2 MECHANICAL FLOW DIAGRAM CONTAINMENT SPRAY SYSTEM FIGURE 6.2.2-2 CONTAINMENT SPRAY PUMP PERFORMANCE CURVES List of Figures 6-xxi | |||
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.2.2-3 REACTOR BLDGS. UNITS 1 & 2 MECHANICAL CONTAINMENT SPRAY SYSTEM PIPING PLAN OF SPRAY PATTERNS FROM C.S. LOOP HEADER A | |||
FIGURE 6.2.2-4 POWERHOUSE-AUXILIARY & REACTOR BLDGS UNITS 1 & 2 MECHANICAL CONTAINMENT SPRAY SYSTEM PIPING FIGURE 6.2.2-5 REACTOR BLDGS. UNITS 1 & 2 MECHANICAL CONTAINMENT SPRAY SYSTEM PIPING PLAN OF SPRAY PATTERNS FROM C.S. LOOP HEADER B FIGURE 6.2.2-6 REACTOR BLDGS. UNITS 1 & 2 MECHANICAL CONTAINMENT SPRAY SYSTEM PIPING SECTION OF SPRAY PATTERNS FROM C.S. LOOP HEADER B FIGURE 6.2.3-1 TYPICAL MECHANICAL PENETRATION SEALS FIGURE 6.2.3-2 TYPICAL PURGE PENETRATION ARRANGEMENT FIGURE 6.2.3-3 TYPICAL ELECTRICAL PENETRATIONS FIGURE 6.2.3-4 AUXILIARY BUILDING ISOLATION BARRIER FIGURE 6.2.3-5 AUXILIARY BUILDING ISOLATION BARRIER FIGURE 6.2.3-6 AUXILIARY BUILDING ISOLATION BARRIER FIGURE 6.2.3-7 AUXILIARY BUILDING ISOLATION BARRIER FIGURE 6.2.3-8 AUXILIARY BUILDING ISOLATION BARRIER FIGURE 6.2.3-9 AUXILIARY BUILDING ISOLATION BARRIER FIGURE 6.2.3-10 AUXILIARY BUILDING ISOLATION BARRIER FIGURE 6.2.3-11 REACTOR BUILDING - UNITS 1 & 2 FLOW DIAGRAM - | |||
HEATING AND VENTILATION AIR FLOW FIGURE 6.2.3-12 POWERHOUSE UNITS 1 & 2 ELECTRICAL LOGIC DIAGRAM - | |||
EMERGENCY GAS TREATMENT SYSTEM FIGURE 6.2.3-13 POWERHOUSE UNITS 1 & 2 ELECTRICAL LOGIC DIAGRAM - | |||
EMERGENCY GAS TREATMENT FIGURE 6.2.3-14 POWERHOUSE UNIT 1 ELECTRICAL LOGIC DIAGRAM - | |||
EMERGENCY GAS TREATMENT FIGURE 6.2.3-15 POWERHOUSE UNITS 1 & 2 ELECTRICAL CONTROL DIAGRAM | |||
- EMERGENCY GAS TREATMENT SYSTEM FIGURE 6.2.3-15-SH-A POWERHOUSE UNIT 2 ELECTRICAL CONTROL DIAGRAM - | |||
EMERGENCY GAS TREATMENT FIGURE 6.2.3-16 POWERHOUSE UNITS 1 & 2 AUXILIARY BUILDING -FLOW DIAGRAM -HEATING & VENTILATING AIR FLOW List of Figures 6-xxii | |||
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.2.3-17A POST-ACCIDENT ANNULUS PRESSURE AND VENT FLOW RATE FIGURE 6.2.3-17 POST-ACCIDENT ANNULUS PRESSURE AND REACTOR UNIT VENT FLOW RATE TRANSIENTS FIGURE 6.2.3-18 REACTOR BUILDING UNITS 1 & 2 MECHANICAL HEATING AND VENTILATING FIGURE 6.2.3-19 REACTOR BUILDING UNITS 1 & 2 MECHANICAL HEATING, VENTILATION, AND AIR CONDITIONING FIGURE 6.2.4-1 TYPE 1, MAIN STEAM X-L3A, X-L3B, X-L3C, X-13D FIGURE 6.2.4-2 TYPE II, FEEDWATER X-12A, X-L2B, X-12C, X-12D FIGURE 6.2.4-3 TYPE III, RESIDUAL HEAT REMOVAL PUMP RETURN X-17, PUMP SUPPLY X-I07 FIGURE 6.2.4-4 TYPE IV AND V (TYPE IV SOCKET WELD ENDS, TYPE V BUTT WELD ENDS) | |||
FIGURE 6.2.4-5 TYPE VI AND VII (TYPE VI FOR SOCKET WELD SS PROCESS LINES, TYPE VII FOR BUTT WELD SS PROCESS LINES) | |||
FIGURE 6.2.4-6 TYPE VIII, FOR BUTT WELD C.S. PROCESS LINES FIGURE 6.2.4-7 TYPE IX, FOR SS PROCESS LINES FIGURE 6.2.4-8 TYPE X, INSTRUMENT PENETRATIONS FIGURE 6.2.4-9 TYPE XII, EMERGENCY SUMP FIGURE 6.2.4-10 TYPE XI, EMERGENCY SUMP FIGURE 6.2.4-11 TYPE XIII, VENTILATION DUCT PENETRATION FIGURE 6.2.4-12 TYPE XIV, EQUIPMENT HATCH FIGURE 6.2.4-13 TYPE XV, PERSONNEL ACCESS FIGURE 6.2.4-14 TYPE XVI, TRANSFER TUBE FIGURE 6.2.4-15 TYPE XVII, INCORE INSTRUMENTATION THIMBLE ASSEMBLY RENEWAL LINE FIGURE 6.2.4-16 TYPE XVIII, ICE BLOWING LINE FIGURE 6.2.4-17 TYPE XIX, ELECTRICAL PENETRATION FIGURE 6.2.4-17A TYPE XX FEEDWATER BYPASS PENETRATIONS X-8A, X-8B, X-8C, X-8D FIGURE 6.2.4-17B TYPE XXI, UPPER AND LOWER CONTAINMENT ERCW SUPPLY AND RETURN CCW FROM EXCESS LETDOWN HEAT EXCHANGER AND FROM PUMP ODOLERS List of Figures 6-xxiii | |||
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.2.4-17C TYPE XXII MULTI LINE PENETRATION X-39 FIGURE 6.2.4-17D TYPE XXIII INSTRUMENT ROOM CHILLED H20 SUPPLY AND RETURN FIGURE 6.2.4-17E TYPE XXIV UHI X-L08, X-109 FIGURE 6.2.4-18 MECHANICAL CONTAINMENT PENETRATION FIGURE 6.2.4-19 POWERHOUSE REACTOR BUILDING UNIT 1 & 2 MECHANICAL SLEEVES-SHIELD BUILDING FIGURE 6.2.4-20 SCHEMATIC DIAGRAM OF LEAKAGE PATHS FIGURE 6.2.4-21 ELECTRICAL LOGIC DIAGRAM CONTAINMENT ISOLATION FIGURE 6.2.4-22A THROUGH 6.2.4-22II DELETED BY AMENDMENT 65 FIGURE 6.2.4-23 ICE BLOWING AND NEGATIVE RETURN LINES - BLIND FLANGE DETAILS FIGURE 6.2.5-1 DELETED BY AMENDMENT 95 FIGURE 6.2.5-2 DELETED BY AMENDMENT 62 FIGURE 6.2.5-3 POWERHOUSE REACTOR BUILDING UNITS 1 & 2 - | |||
MECHANICAL HEATING, VENTILATING AND AIR CONDITIONING FIGURE 6.2.5-4 POWERHOUSE REACTOR BUILDING UNITS 1 & 2 - | |||
MECHANICAL HEATING, VENTILATING AND AIR CONDITIONING FIGURE 6.2.5-5 POWERHOUSE REACTOR BUILDING UNITS 1 & 2 - | |||
MECHANICAL HEATING, VENTILATION AND AIR CONDITIONING FIGURE 6.2.5-6 SAMPLE LOOP FLOW DIAGRAM FIGURE 6.2.5-7 DELETED BY AMENDMENT 95 FIGURE 6.2.5-7A DELETED BY AMENDMENT 95 FIGURE 6.2.5-8 IGNITER LOCATIONS - LOWER COMPARTMENT AND DEAD ENDED COMPARTMENTS FIGURE 6.2.5-9 IGNITER LOCATIONS - LOWER COMPARTMENTS FIGURE 6.2.5-10 IGNITER LOCATIONS - UPPER PLENUM AND UPPER COMPARTMENTS FIGURE 6.2.5-11 IGNITER LOCATIONS - DOME FIGURE 6.2.5-12 IGNITER LOCATIONS - ELEVATION FIGURE 6.3-1-1 POWERHOUSE UNIT 1 SAFETY INJECTION SYSTEM - FLOW DIAGRAM List of Figures 6-xxiv | |||
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.3-1-2 POWERHOUSE UNIT 1 & 2 ELECTRICAL CONTROL DIAGRAM | |||
- SAFETY INJECTION SYSTEM FIGURE 6.3-1-2-SH-A POWERHOUSE UNIT 1 ELECTRICAL CONTROL DIAGRAM - | |||
SAFETY INJECTION SYSTEM FIGURE 6.3-1-3 POWERHOUSE UNIT 1 ELECTRICAL CONTROL DIAGRAM SAFETY INJECTION FIGURE 6.3-1-3-SH-A POWERHOUSE UNIT 2 ELECTRICAL CONTROL DIAGRAM - | |||
SAFETY INJECTION FIGURE 6.3-1-3-SH-B POWERHOUSE UNIT 1 ELECTRICAL CONTROL DIAGRAM - | |||
SAFETY INJECTION FIGURE 6.3-2 UNIT 2 - PERFORMANCE CURVES FOR THE RESIDUAL HEAT REMOVAL PUMPS FIGURE 6.3-3 PERFORMANCE CURVES FOR THE SAFETY INJECTION PUMPS FIGURE 6.3-4 PERFORMANCE CURVES FOR THE CHARGING PUMPS FIGURE 6.3-5 SHEETS 1 AND 2, DELETED BY AMENDMENT 63 FIGURE 6.3-6 CONTAINMENT SUMP FIGURE 6.3-6A CONTAINMENT SUMP FIGURE 6.5-1 ICE CONDENSER FIGURE 6.7-1 ISOMETRIC OF ICE CONDENSER FIGURE 6.7-2 FLOOR STRUCTURE FIGURE 6.7-3 WEAR SLAB TOP SURFACE AREA SHOWING TYPICAL COOLANT PIPING LAYOUT FIGURE 6.7-4 LATTICE FRAME ORIENTATION FIGURE 6.7-5 LOAD DISTRIBUTION FOR TANGENTIAL SEISMIC AND BLOWDOWN LOADS IN ANALYTICAL MODEL FIGURE 6.7-6 LATTICE FRAME FIGURE 6.7-7 LATTICE FRAME ANALYSIS MODEL FIGURE 6.7-8 TYPICAL BOTTOM ICE BASKET ASSEMBLY FIGURE 6.7-9 COMBINATIONS OF CONCENTRIC AXIAL LOAD AND DISTRIBUTION LOAD THAT WILL CAUSE FAILURE OF A PERFORATED METAL ICE CONDENSER BASKET MATERIAL FIGURE 6.7-10 CRANE ASSEMBLY FIGURE 6.7-11 CRANE RAIL ASSEMBLY FIGURE 6.7-12 REFRIGERANT CYCLE DIAGRAM List of Figures 6-xxv | |||
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.7-13 GLYCOL CYCLE TO EACH CONTAINMENT FIGURE 6.7-14 SCHEMATIC FLOW DIAGRAMS OF AIR COOLING CYCLE FIGURE 6.7-15 AIR HANDLING UNIT SUPPORT STRUCTURE FIGURE 6.7-16 FLOW AREA - PRESSURE DIFFERENTIAL FIGURE 6.7-17 LOWER INLET DOOR ASSEMBLY FIGURE 6.7-18 DETAILS OF LOWER INLET DOOR SHOWING HINGE, PROPORTIONING MECHANISM LIMIT SWITCHES AND SEALS FIGURE 6.7-19 INLET DOOR FRAME ASSEMBLY FIGURE 6.7-20 INLET DOOR PANEL ASSEMBLY FIGURE 6.7-21 LOWER INLET DOOR SHOCK ABSORBER ASSEMBLY FIGURE 6.7-22 FOUR LOOP ICE CONDENSER LOWER SUPPORT STRUCTURE CONCEPTUAL PLAN AND SECTIONS FIGURE 6.7-23 FOUR LOOP ICE CONDENSER LOWER SUPPORT STRUCTURE GENERAL ASSEMBLY FIGURE 6.7-24 ANTS MODEL ASSEMBLY FIGURE 6.7-25 FINITE ELEMENT MODEL OF PORTAL FRAME FIGURE 6.7-26 SCHEMATIC DIAGRAM OF FORCES APPLIED TO THREE PIER LOWER SUPPORT STRUCTURE FIGURE 6.7-27 FORCE TRANSIENT HOT LEG BREAK FIGURE 6.7-28 DLF SPECTRA HOT LEG BREAK FORCE TRANSIENT FIGURE 6.7-29 TOP DECK TEST ASSEMBLY FIGURE 6.7-30 DETAILS OF TOP DECK DOOR ASSEMBLY FIGURE 6.7-31 INTERMEDIATE DECK DOOR ASSEMBLY FIGURE 6.7-32 AIR DISTRIBUTION DUCT FIGURE 6.7-33 AIR DISTRIBUTION DUCT FIGURE 6.7-34 PHASE DIAGRAM FOR NA2 B4 07.10 H2O/WATER SYSTEM AT ONE ATMOSPHERE FIGURE 6.7-35 ICE BED COMPACTION VERSUS TIME FIGURE 6.7-36 TEST ICE BED COMPACTION VERSUS ICE BED HEIGHT FIGURE 6.7-37 TOTAL ICE COMPACTION VERSUS ICE BED HEIGHT FIGURE 6.7-38 ICE CONDENSER RTD LOCATION FIGURE 6.7-39 BLOCK DIAGRAM ICE CONDENSER TEMPERATURE MONITORING SYSTEM FIGURE 6.7-40 DOOR MONITORING ZONES List of Figures 6-xxvi | |||
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.7-41 POWERHOUSE UNIT 1 WIRING DIAGRAMS ICE CONDENSER SYSTEM SCHEMATIC DIAGRAMS FIGURE 6.7-42 DELETED BY AMENDMENT 89 FIGURE 6.7-43 DELETED BY AMENDMENT 89 FIGURE 6.7-44 MODEL OF HORIZONTAL LATTICE FRAME STRUCTURE FIGURE 6.7-45 GROUP OF SIX INTERCONNECTED LATTICE FRAMES FIGURE 6.7-46 LATTICE FRAME LCE BASKET GAP FIGURE 6.7-47 TYPICAL DISPLACEMENT TIME HISTORIES FOR 12-FOOT BASKET WITH END SUPPORTS - PLUCK TEST FIGURE 6.7-48 NON LINEAR DYNAMIC MODEL FIGURE 6.7-49 3-MASS TANGENTIAL ICE BASKET MODEL FIGURE 6.7-50 9-MASS RADIAL ICE BASKET MODEL FIGURE 6.7-51 48-FOOT BEAM MODEL FIGURE 6.7-52 PHASING MASS MODEL OF ADJACENT LATTICE FRAME BAYS FIGURE 6.7-53 PHASING STUDY MODEL, 1 LEVEL LATTICE FRAME 300 DEGREES NON-LINEAR MODEL FIGURE 6.7-54 TYPICAL CRANE WALL DISPLACEMENT FIGURE 6.7-55 TYPICAL ICE BASKET DISPLACEMENT RESPONSE FIGURE 6.7-56 TYPICAL ICE BASKET IMPACT FORCE RESPONSE FIGURE 6.7-57 TYPICAL CRANE WALL PANEL LOAD RESPONSE FIGURE 6.7-58 WALL PANEL DESIGN LOAD DISTRIBUTION OBTAINED USING THE 48-FOOT BEAM MODEL TANGENTIAL CASE FIGURE 6.7-59 WALL PANEL DESIGN LOAD DISTRIBUTION OBTAINED USING THE 48-FOOT BEAM MODEL RADIAL CASE List of Figures 6-xxvii | |||
WATTS BAR LIST OF FIGURES Section Title THIS PAGE INTENTIONALLY BLANK List of Figures 6-xxviii | |||
WATTS BAR WBNP-112 06-1_Part_01_of_02_LTR.pdf 6.0 ENGINEERED SAFETY FEATURES 6.1 ENGINEERED SAFETY FEATURE MATERIALS 6.1.1 Metallic Materials 6.1.1.1 Materials Selection and Fabrication Typical material specifications used for the principal pressure retaining applications in components in the Engineered Safety Features (ESF) are listed inTable 5.2-9. All materials utilized are procured in accordance with the material specification requirements of the ASME Boiler and Pressure Vessel Code, Section III, plus applicable and appropriate Addenda and Code Cases. | |||
The welding materials used for joining the ferritic base materials of the ESF conform to, or are equivalent to, ASME Material Specifications SFA 5.1, 5.2, 5.5, 5.17, 5.18, and 5.20. The welding materials used for joining nickel-chromium-iron alloy in similar base material combination and in dissimilar ferritic or austenitic base material combination conform to ASME Material Specifications SFA 5.11 and 5.14. The welding materials used for Joining the austenitic stainless steel base materials conform to ASME Material Specifications SFA 5.4 and 5.9. These materials are tested and qualified to the requirements of the ASME Code, Section III and Section IX rules and are used in procedures which have been qualified to these same rules. The methods utilized to control delta ferrite content in austenitic stainless steel weldments are discussed in Section 5.2.5.7. | |||
The parts of components in contact with borated water are fabricated of or clad with austenitic stainless steel or equivalent corrosion resistant material [Ref. 4]. The integrity of the safety-related components of the ESF is maintained during all stages of component manufacture. Austenitic stainless steel is utilized in the final heat treated condition as required by the respective ASME Code Section II material specification for the particular type or grade of alloy. Furthermore, it is required that austenitic stainless steel materials used in the ESF components be handled, protected, stored, and cleaned according to recognized and accepted methods which are designed to minimize contamination which could lead to stress corrosion cracking. The rules covering these controls are stipulated in Westinghouse process specifications, which are discussed in Section 5.2.5.1. Additional information concerning austenitic stainless steel, including the avoidance of sensitization and the prevention of intergranular attack, can be found in Section 5.2.5. No cold worked austenitic stainless steels having yield strengths greater than 90,000 psi are used for components of the ESF within the Westinghouse standard scope. | |||
Westinghouse supplied components within the containment that would be exposed to core cooling water and containment sprays in the event of a loss-of-coolant accident utilize materials listed in Table 5.2-9. These components are manufactured primarily of stainless steel or other corrosion resistant, high temperature material. The integrity of the materials of construction for ESF equipment when exposed to post design basis accident (DBA) conditions has been evaluated. Post-DBA conditions were ENGINEERED SAFETY FEATURE MATERIALS 6.1-1 | |||
WATTS BAR WBNP-112 conservatively represented by test conditions. The test program[1] performed by Westinghouse considered spray and core cooling solutions of the design chemical compositions, as well as the design chemical compositions contaminated with corrosion and deterioration products which may be transferred to the solution during recirculation. The effects of sodium (free caustic), chlorine (chloride), and fluorine (fluoride) on austenitic stainless steels were considered. Based on the results of this investigation, as well as testing by ORNL and others, the behavior of austenitic stainless steels in the post-DBA environment will be very acceptable. No cracking is anticipated on any equipment even in the presence of postulated levels of contaminants, provided the core cooling and spray solution pH is maintained at an adequate level. The inhibitive properties of alkalinity (hydroxyl ion) against chloride cracking and the inhibitive characteristic of boric acid on fluoride cracking have been demonstrated. Note that qualified coatings inside primary containment located within the zone of influence are assumed to fail for the analysis in the event of a loss-of-coolant accident. The zone of influence for qualified coatings is defined as a spherical zone with a radius of 10 times the break diameter. Coatings on exposed surfaces outside the zone of influence within the containment are not subject to breakdown under exposure to the spray solution and can withstand the temperature and pressure expected in the event of a loss-of-coolant accident. | |||
6.1.1.2 Composition, Compatibility, and Stability of Containment and Core Spray Coolants The vessels used for storing ESF coolants include the accumulators and the refueling water storage tank. | |||
The accumulators are carbon steel clad with austenitic stainless steel [Ref. 4]. | |||
Because of the corrosion resistance of these materials, significant corrosive attack on the storage vessels is not expected. | |||
The accumulators are vessels filled with borated water and pressurized with nitrogen gas. The nominal boron concentration, as boric acid, is 3150 ppm. Samples of the solution in the accumulators are taken periodically for checks of boron concentration. | |||
Principal design parameters of the accumulators are listed in Table 6.3-1. | |||
The refueling water storage tank is a source of borated cooling water for injection. The nominal boron concentration, as boric acid, is 3200 ppm . The temperature of the refueling water is maintained above the solubility limit for the maximum boron concentration. Principal design parameters of the refueling water storage tank are given in Section 9.2.7. | |||
The ice in the ice condenser is borated by adding sodium tetraborate to the ice. The aqueous solution resulting from the melted ice has a nominal boron concentration of 1900 +100 ppm. In the event of an accident, this solution would be delivered to the containment sump. Containment sump pH is also controlled by the sodium tetraborate in the ice. The pH of the ice is maintained between 9.0 and 9.5, which results in a sump pH of at least 7.5. | |||
6.1-2 ENGINEERED SAFETY FEATURE MATERIALS | |||
WATTS BAR WBNP-112 Information concerning hydrogen release by the corrosion of containment metals and the control of the hydrogen and combustible gas concentrations within the containment following a LOCA is discussed in Section 6.2.5. | |||
6.1.2 Organic Materials For paints and coatings inside containment, the conformance with Regulatory Guide 1.54 is described in Section 6.1.4. | |||
Organic materials within the primary containment are identified and quantified according to the following categories: electrical insulation, surface coatings, miscellaneous ALARA (catch basin), containment and shielding (lead blankets), ice condenser equipment, and identification tags for valves and instruments. There is no asphalt inside containment. There is a small amount of wood (roughly 215 lbs) located inside the ice condenser. The effects of elastomers and plastic on hydrogen generation have been evaluated and determined to be inconsequential. Therefore, the quantities identified below are considered historical and need not be revised due to design changes. | |||
The information in this section is based on a single reactor unit. | |||
6.1.2.1 Electrical Insulation The typical types of electrical cable insulation/jacket material that are utilized within the primary containment are: silcon rubber, polyethylene, ethylene rubber, chlorosulfonated polyethlene, polylefin, cross linked polyethlene, kapton. These materials are not significant contributors to hydrongen generation during a design basis accident (approximately 28,000 lbs). | |||
6.1.2.2 Surface Coatings Material Mass, lbs Concrete Surfaces: | |||
Epoxy 2070 Phenolic-epoxy 300 Steel Surfaces: | |||
Phenolic-epoxy 1810 Steel surfaces are undercoated with approximately 85% zinc in a silicate binder (carbozinc 11), or epoxy, such as Amerlock 400. | |||
Protective coatings for use in the reactor containment have been evaluated as to their suitability in post-DBA conditions. Tests have shown that the epoxy and modified phenolic systems are the most desirable of the generic types evaluated for in-containment use. This evaluation considered resistance to high temperature and chemical conditions anticipated following a LOCA, as well as high radiation resistance | |||
[Ref. 2]. Coating systems qualified as CSL-1, for one plant may be used by the other ENGINEERED SAFETY FEATURE MATERIALS 6.1-3 | |||
WATTS BAR WBNP-112 plants provided the applicable DBA requirements for the area where it is to be used are enveloped by the qualification testing system. These requirements include but are not limited to temperature, pressure, radiation and spray solution. | |||
6.1.2.3 Ice Condenser Equipment Material Mass, lbs Lower Door Seals (Styrene butadiene) 530 Equipment Access Door Seals (Natural rubber) 5 Vent curtain (Laminated mylar) 5 Ice Condenser Seal: | |||
Natural Rubber 600 Nylon 360 Miscellaneous Washers: | |||
Noryl SEIOO (phenylene oxide) 50 Gasketing Material: | |||
Neoprene 5060 Drain Line Expansion Joint 6.1.2.4 Identification Tags Material Mass, lbs Valves: | |||
ABS (acrylonitrile-butadiene-styrene) 50 Instruments: | |||
ABS (acylonitrile-butadiene-styrene) 30 6.1.2.5 Valves and Instruments within Containment Material Mass, lbs Diaphragms, O-Rings, Solenoid Seals: | |||
Buna-N (acrylonitrile-Butadiene) 130 6.1-4 ENGINEERED SAFETY FEATURE MATERIALS | |||
WATTS BAR WBNP-112 6.1.2.6 Heating and Ventilating Door Seals Material Mass, lbs Neoprene (chloroprene) 100 6.1.2.7 Miscellaneous Material Mass, lbs Catch Basins (polyethylene) 100 Lead Shielding Blankets (Hypalon, Vinyl, 1200 Methyllpolysiloxance) 6.1.3 Post-Accident Chemistry Following a LOCA, the emergency core cooling solution recirculated in containment is composed of boric acid (H3BO3) from the reactor coolant, refueling water storage tank (RWST), cold leg accumulators and affected injection piping, lithium hydroxide (LiOH) from the reactor coolant and sodium tetraborate (Na2B4O7) from the ice in the ice condenser. | |||
6.1.3.1 Boric Acid, H3BO3 Boric acid up to a maximum concentration of 3300 ppm boron, can be found in the reactor coolant loop (4 loops, reactor vessel, pressurizer), and boric acid at a maximum concentration of 3300 ppm boron is found in the cold leg injection accumulators, the refueling water storage tank, and in associated piping. This limit may be exceeded during Mode 6 operation. These subsystems, when at maximum volume, represent a total mass of boric acid in the amount of 93,928 pounds. | |||
6.1.3.2 Lithium Hydroxide Lithium Hydroxide at a maximum concentration of 7.6 ppm lithium is found in the reactor coolant system for pH control. | |||
6.1.3.3 Sodium Tetraborate Sodium tetraborate is an additive in the ice stored in the ice condenser for the purpose of maintaining containment sump pH of at least 7.5 after all the ice has melted. | |||
The minimum amount of ice assumed in the Post-LOCA sump pH analysis is 2.26 x 106 lbs [Ref. 3]. Boric acid and NaOH are formed during ice melt following a LOCA according to the following equation: | |||
Na 2 B 4 O 7 + 7H 2 O 2NaOH + 4H 3 BO 3 ENGINEERED SAFETY FEATURE MATERIALS 6.1-5 | |||
WATTS BAR WBNP-112 6.1.3.4 Final Post-Accident Chemistry The final post-accident sump pH is greater than 7.5. The estimated sump pH versus time calculation indicates that the post-LOCA sump pH remains within the allowable range of 7.5 to 10.0 for the duration of the event. | |||
6.1.4 Degree of Compliance with Regulatory Guide 1.54 for Paints and Coatings Inside Containment TVA is committed to adhere to Appendix B of 10 CFR 50 and ANSI N45.2 as required to produce a quality end product. Basically, it is TVA's position that the Quality Assurance Program (QA) for protective coatings inside the containment should control four activities in the coating program. The four major areas to be controlled are: | |||
(1) The coating material itself, by extending requirements on the manufacturing process and qualification of coating systems through the use of applicable portions of ANSI Standards N101.2 and N512. | |||
(2) The preparation of the surface to which coatings are to be applied. | |||
(3) The inspection process. | |||
(4) The application of the coating systems. | |||
All four of these controlled activities have appropriate documentation and records to meet Appendix B requirements. | |||
TVA agrees with Regulatory Guide 1.54, except the endorsement to ANSI N101.4 in paragraph C.1. | |||
TVA's protective coating application program within the containment is in conformance with Appendix B to 10 CFR 50 and ANSI N45.2. In addition, applicable provisions found in ANSI N101.4 have been incorporated into TVA surface preparation, coating application/inspection specifications, and coating QA procedures. | |||
Unqualified/uncontrolled coatings are accounted for and maintained within the limits specified in the analysis for containment coatings and in the transport analysis for the zone of influence. The zone of influence is defined as that area at the water surface into which a falling paint particle does not settle to the bottom, but rather, is transported to the sump strainer assembly by the flow of water. | |||
REFERENCES (1) WCAP-7803, "Behavior of Austenitic Stainless Steel in Post Hypothetical Loss of Coolant Environment." | |||
(2) WCAP-7825, "Evaluation of Protective Coatings for Use in Reactor Containment." | |||
6.1-6 ENGINEERED SAFETY FEATURE MATERIALS | |||
WATTS BAR WBNP-112 (3) WBT-D-1413, Response to Comments on FSAR Mark-ups, dated January 7, 2010. | |||
(4) TVAs letter to NRC dated July 30, 2003, Petition Pursuant to 10 CFR 2.206 | |||
- Reactor Coolant System Stainless Steel Cladding. (Unit 1) | |||
ENGINEERED SAFETY FEATURE MATERIALS 6.1-7 | |||
WATTS BAR WBNP-112 Table 6.1-1 Deleted by Amendment 97 6.1-8 ENGINEERED SAFETY FEATURE MATERIALS | |||
Deleted by Amendment 97 WATTS BAR ENGINEERED SAFETY FEATURE MATERIALS 6.1-9 Figure 6.1-1 Deleted by Amendment 97 WBNP-112 | |||
WATTS BAR WBNP-112 THIS PAGE INTENTIONALLY BLANK 6.1-10 ENGINEERED SAFETY FEATURE MATERIALS | |||
WATTS BAR WBNP-112 6.2 CONTAINMENT SYSTEMS 6.2.1 Containment Functional Design 6.2.1.1 Design Bases 6.2.1.1.1 Primary Containment Design Bases The containment is designed to assure that an acceptable upper limit of leakage of radioactive material is not exceeded under design basis accident conditions. For purposes of integrity, the containment may be considered as the containment vessel and containment isolation system. This structure and system are directly relied upon to maintain containment integrity. The emergency gas treatment system and Reactor Building function to keep out-leakage minimal (the Reactor Building also serves as a protective structure), but are not factors in determining the design leak rate. | |||
The containment is specifically designed to meet the intent of the applicable General Design Criteria listed in Section 3.1. This section, Chapter 3, and other portions of Chapter 6 present information showing conformance of design of the containment and related systems to these criteria. | |||
The ice condenser is designed to limit the containment pressure below the design pressure for all reactor coolant pipe break sizes up to and including a double-ended severance. Characterizing the performance of the ice condenser requires consideration of the rate of addition of mass and energy to the containment as well as the total amounts of mass and energy added. Analyses have shown that the accident which produces the highest blowdown rate into a condenser containment will result in the maximum containment pressure rise; that accident is the double-ended guillotine or split severance of a reactor coolant pipe. The design basis accident for containment analysis based on sensitivity studies is therefore the double-ended guillotine severance of a reactor coolant pipe at the reactor coolant pump suction. Post-blowdown energy releases can also be accommodated without exceeding containment design pressure. | |||
The functional design of the containment is based upon the following accident input source term assumptions and conditions: | |||
(1) The design basis blowdown energy of 314.9 x 106 Btu and mass of 498.1 x 103 lb put into the containment. (See Section 6.2.1.3.6) | |||
(2) A core power of 3411 MWt (plus 2% allowance for calorimetric error). (See Section 6.2.1.3.6) | |||
Containment Functional Design 6.2.1-1 | |||
WATTS BAR WBNP-112 (3) The minimum engineered safety features are (i.e., the single failure criterion applied to each safety system) comprised of the following: | |||
(a) The ice condenser which condenses steam generated during a LOCA, thereby limiting the pressure peak inside the containment (see Section 6.7). | |||
(b) The containment isolation system which closes those fluid penetrations not serving accident-consequence limiting purposes (see Section 6.2.4). | |||
(c) The containment spray system which sprays cool water into the containment atmosphere, thereby limiting the pressure peak (particularly in the long term - see Section 6.2.2). | |||
(d) The emergency gas treatment system (EGTS) which produces a slightly negative pressure within the annulus, thereby precluding out-leakage and relieving the post-accident thermal expansion of air in the annulus (see Section 6.5.1). | |||
(e) The air return fans which return air to the lower compartment (See Section 6.8). | |||
Consideration is given to subcompartment differential pressure resulting from a design basis accident discussed in Sections 3.8.3.3, 6.2.1.3.9, and 6.2.1.3.4. If a design basis accident were to occur due to a pipe rupture in these relatively small volumes, the pressure would build up at a faster rate than in the containment, thus imposing a differential pressure across the wall of these structures. | |||
Parameters affecting the assumed capability for post-accident pressure reduction are discussed in Section 6.2.1.3.3. | |||
Three events that may result in an external pressure on the containment vessel have been considered: | |||
(1) Rupture of a process pipe where it passes through the annulus. | |||
(2) Inadvertent air return fan operation during normal operation. | |||
(3) Inadvertent containment spray system initiation during normal operation. | |||
The design of the guard pipe portion of hot penetrations is such that any process pipe leakage in the annulus is returned to the containment. All process piping which has potential for annulus pressurization upon rupture is routed through hot penetrations. | |||
Section 6.2.4 discusses hot penetrations. | |||
Inadvertent air return fan operation during normal operation opens the ice condenser lower inlet doors, which in turn, results in sounding an alarm in the MCR. Sufficient 6.2.1-2 Containment Functional Design | |||
WATTS BAR WBNP-112 time exists for operator action to terminate fan operation prior to exceeding the containment design external pressure. | |||
The logic and control circuits of the containment spray system are such that inadvertent containment spray would not take place with a single failure. The spray pump must start and the isolation valve must open before there can be any spray. In addition, the Watts Bar containment is so designed that even if an inadvertent spray occurs, containment integrity is preserved without the use of a vacuum relief. | |||
The containment spray system is automatically actuated by a hi-hi containment pressure signal from the solid state protection system (SSPS). To prevent inadvertent automatic actuation, four comparator outputs, one from each protection set are processed through two coincidence gates. Both coincidence gates are required to have at least two high inputs before the output relays, which actuate the containment spray system, are energized. Separate output relays are provided for the pump start logic and discharge valve open logic. Additional protection is provided by an interlock between the pump and discharge valve, which requires the pump to be running before the discharge valve will automatically open. | |||
Section 3.8.2 describes the structural design of the containment vessel. The containment vessel is designed to withstand a net external pressure of 2.0 psi. The containment vessel is designed to withstand the maximum expected net external pressure in accordance with ASME Boiler and Pressure and Vessel Code Section III, paragraph NE-7116. | |||
6.2.1.2 Primary Containment System Design The containment consists of a containment vessel and a separate Shield Building enclosing an annulus. The containment vessel is a freestanding, welded steel structure with a vertical cylinder, hemispherical dome, and a flat circular base. The Shield Building is a reinforced concrete structure similar in shape to the containment vessel. The design of these structures is described in Section 3.8. | |||
The design internal pressure for the containment is 13.5 psig, and the design temperature is 250°F. The design basis leakage rate is 0.25 weight percent/24 hr. The design methods to assure integrity of the containment internal structures and sub-compartments from accident pressure pulses are described in Section 3.8. | |||
6.2.1.3 Design Evaluation 6.2.1.3.1 Primary Containment Evaluation (1) The leaktightness aspect of the secondary containment is discussed in Section 6.2.3. The primary containment's leaktightness does not depend on the operation of any continuous monitoring or compressor system. The leak testing of the primary containment and its isolation system is discussed in Section 6.2.6. | |||
Containment Functional Design 6.2.1-3 | |||
WATTS BAR WBNP-112 (2) The acceptance criteria for the leaktightness of the primary containment are such that at containment design pressure, there is a 25% margin between the acceptable maximum leakage rate and the maximum permissible leakage rate. | |||
6.2.1.3.2 General Description of Containment Pressure Analysis The time history of conditions within an ice condenser containment during a postulated loss of coolant accident can be divided into two periods for calculation purposes: | |||
(1) The initial reactor coolant blowdown, which for the largest assumed pipe break occurs in approximately 10 seconds. | |||
(2) The post blowdown phase of the accident which begins following the blowdown and extends several hours after the start of the accident. | |||
During the first few seconds of the blowdown period of the reactor coolant system, containment conditions are characterized by rapid pressure and temperature transients. It is during this period that the peak transient pressures, differential pressures, temperature and blowdown loads occur. To calculate these transients a detailed spatial and short time increment analysis was necessary. This analysis was performed with the Transient Mass Distribution (TMD) computer code (Reference 4) with the calculation time of interest extending up to a few seconds following the accident initiation (See Section 6.2.1.3.4). | |||
Physically, tests at the ice condenser Waltz Mill test facility have shown that the blowdown phase represents that period of time in which the lower compartment air and a portion of the ice condenser air are displaced and compressed into the upper compartment and the remainder of the ice condenser. The containment pressure at or near the end of blowdown is governed by this air compression process. The containment compression ratio calculation is described in Section 6.2.1.3.4. | |||
Containment pressure during the post blowdown phase of the accident is calculated with the LOTIC code which models the containment structural heat sinks and containment safeguards systems. | |||
6.2.1.3.3 Long-Term Containment Pressure Analysis Early in the ice condenser development program it was recognized that there was a need for modeling of long-term ice condenser containment performance. It was realized that the model would have to have capabilities comparable to those of the dry containment (COCO) model. These capabilities would permit the model to be used to solve problems of containment design and optimize the containment and safeguards systems. This has been accomplished in the development of the LOTIC code[1]. | |||
The model of the containment consists of five distinct control volumes; the upper compartment, the lower compartment, the portion of the ice bed from which the ice has melted, the portion of the ice bed containing unmelted ice, and the dead ended compartments. The ice condenser control volume with unmelted ice is further 6.2.1-4 Containment Functional Design | |||
WATTS BAR WBNP-112 subdivided into six subcompartments to allow for maldistribution of break flow to the ice bed. | |||
The conditions in these compartments are obtained as a function of time by the use of fundamental equations solved through numerical techniques. These equations are solved for three distinct phases in time. Each phase corresponds to a distinct physical characteristic of the problem. Each of these phases has a unique set of simplifying assumptions based on test results from the ice condenser test facility. These phases are the blowdown period, the depressurization period, and the long term. | |||
The most significant simplification of the problem is the assumption that the total pressure in the containment is uniform. This assumption is justified by the fact that after the initial blowdown of the reactor coolant system, the remaining mass and energy released from this system into the containment are small and very slowly changing. The resulting flow rates between the control volumes will also be relatively small. These small flow rates then are unable to maintain significant pressure differences between the compartments. | |||
In the control volumes, which are always assumed to be saturated, steam and air are assumed to be uniformly mixed and at the control volume temperature. The air is considered a perfect gas, and the thermodynamic properties of steam are taken from the ASME steam table. | |||
For the purpose of calculation, the condensation of steam is assumed to take place in a condensing node located between the two control volumes in the ice storage compartment. | |||
Containment Pressure Calculation The following are the major input assumptions used in the LOTIC analysis for the pump suction pipe rupture case with the steam generators considered as an active heat source for the Watts Bar Nuclear Plant containment: | |||
(1) Minimum safeguards are employed in all calculations, e.g., one of two spray pumps and one of two spray heat exchangers; one of two RHR pumps and one of two RHR heat exchangers providing flow to the core; one of two safety injection pumps and one of two centrifugal charging pumps; and one of two air return fans. | |||
(2) 2.26 x 106 lbs. of ice initially in the ice condenser which is at 15°F. | |||
(3) The blowdown, reflood, and post reflood mass and energy releases described in Section 6.2.1.3.6 were used. | |||
(4) Blowdown and post-blowdown ice condenser drain temperatures of 190°F and 130°F are used[5]. | |||
(5) Nitrogen from the accumulators in the amount of 2955.68 lbs. included in the calculations. | |||
Containment Functional Design 6.2.1-5 | |||
WATTS BAR WBNP-112 (6) Essential raw cooling water temperature of 88°F is used on the spray heat exchanger and the component cooling heat exchanger. Note: The containment analysis was run at an ERCW temperature of 88°F although the containment spray, component cooling, and residual heat removal heat exchanger UA values are based on an ERCW temperature of 85°F to provide additional conservatism. | |||
(7) The air return fan is effective 10 minutes after the transient is initiated. The actual air return fan initiation can take place in 9 + 1 minutes, with initiation as early as 8 minutes not adversely affecting the analysis results. | |||
(8) No maldistribution of steam flow to the ice bed is assumed. | |||
(9) No ice condenser bypass is assumed. (This assumption depletes the ice in the shortest time and is thus conservative.) | |||
(10) The initial conditions in the containment are a temperature of 120°F in the lower and dead-ended volumes, 110°F in the upper volume, and 15°F in the ice condenser. All volumes are at a pressure of 0.3 psig and a 10-percent relative humidity, except the ice condenser which is at 100-percent relative humidity. | |||
(11) A containment spray pump flow of 4000 gpm is used in the upper compartment. The analyzed diesel loading sequence for the containment sprays to energize and come up to full flow and head in 234 seconds is tabulated in Table 6.2.1-25. | |||
(12) A residual spray (2000 gpm design, 1475 gpm analytical) is used. The residual heat removal pump and spray pump take suction from the sump during recirculation. | |||
During the recirculation phase of a LOCA mass and energy release transient, a portion of the RHR pump flow can be diverted to the RHR sprays. The minimum time before RHR spray can be placed in service, as indicated in the Watts Bar Nuclear Plant System Description N3-72-4001, R19, Containment Heat Removal Spray System, is at least 1 hour after LOCA initiation to ensure adequate RHR flow to the core to remove the initial decay heat. Based on the preceding criteria, the RHR spray initiation was modeled at 4346.7 seconds into the LOCA containment response transient. | |||
A discussion of the core cooling capability of the emergency core cooling system is given in Section 6.3.1 for this mode of operation. | |||
(13) Containment structural heat sink data is found in Table 6.2.1-1. (Note: The dead-ended compartment structural heat sinks were conservatively neglected.) | |||
6.2.1-6 Containment Functional Design | |||
== | WATTS BAR WBNP-112 (14) The operation of one containment spray heat exchanger (UA = 2.44 x 106 Btu/hr-°F incorporating a 10% tube plugging margin) for containment cooling and the operation of one RHR heat exchanger (UA = 1.496 x 106 Btu/hr-°F) for core cooling. The component cooling system heat exchanger UA was modeled at 5.778 x 106 Btu/hr-°F. | ||
(15) The air return fan returns air at a rate of 40,000 cfm from the upper to lower compartment. | |||
(16) An active sump volume of 51,000 ft3 is used. | |||
(17) The pump flowrates vs. time given in Table 6.2.1-2 were used in support of RWST draindown. (These flow values reflect ECCS pumps at runout against the design containment pressure, using the minimum composite pump curves shown in Figures 6.3-2, 6.3-3, and 6.3-4, which are degraded by 5% | |||
and bound what is achievable in the plant. Switchover times from injection to recirculation that are achievable in the plant for each ECCS pump were conservatively modeled in the analysis.) | |||
(18) A power rating of 102% of licensed core power (3411 MWt) is assumed, but not explicitly modeled. [Decay heat is based on a reactor power of 3479.22 MWt (+2%) for mass and energy release computations. See Section 6.2.1.3.6.] | |||
(19) Hydrogen gas was added to the containment in the amount of 25,230.2 Standard Cubic Feet (SCF) over 24 hours. Sources accounted for were radiolysis in the core and sump post-LOCA, corrosion of plant materials (aluminum, zinc, and painted surfaces found in containment), reaction of 1% | |||
of the Zirconium fuel rod cladding in the core, and hydrogen gas assumed to be dissolved in the reactor coolant system water. (This bounds tritium producing core designs.) | |||
(20) The containment compartment volumes were based on the following: upper compartment 645,818 ft3, lower compartment 221,074 ft3, and dead-ended compartment 146,600 ft3. (Note: These volumes represent TMD volumes. | |||
For Containment Integrity Analysis, the volumes are adjusted to maximize air mass and the compression ratio.) | |||
(21) Subcooling of emergency core cooling (ECC) water from the RHR heat exchanger is assumed. | |||
(22) Essential raw cooling water flow to the containment spray heat exchanger was modeled as 5,200 gpm. Also, the essential raw cooling water flow to the component cooling heat exchanger was modeled as 6,250 gpm. | |||
(23) The decay heat curve used to calculate mass and energy releases after steam generator equilibration is the same as presented in the mass and energy release section of the FSAR (subsection 6.2.1.3.6). | |||
Containment Functional Design 6.2.1-7 | |||
WATTS BAR WBNP-112 With these assumptions, the heat removal capability of the containment is sufficient to absorb the energy releases and still keep the maximum calculated pressure well below design. | |||
The following plots are provided: | |||
Figure 6.2.1-1, Containment Pressure Versus Time Figure 6.2.1-2a, Upper Compartment Temperature Versus Time Figure 6.2.1-2b, Lower Compartment Temperature Versus Time Figure 6.2.1-3, Active and Inactive Sump Temperature Transients Figure 6.2.1-4, Melted Ice Mass Transient Figure 6.2.1-4a, Comparison of Containment Pressure Versus Ice Melt Tables 6.2.1-3 and 6.2.1-4 give energy accountings at various points in the transient. | |||
As can be seen from Figure 6.2.1-1 the maximum calculated Containment pressure is 12.86 psig, occurring at approximately 4348 seconds. | |||
Structural Heat Removal Provision is made in the containment pressure analysis for heat storage in interior and exterior walls. Each wall is divided into a number of nodes. For each node, a conservation of energy equation expressed in finite difference forms accounts for transient conduction into and out of the node and temperature rise of the node. Table 6.2.1-1 is a summary of the containment structural heat sinks used in the analysis. The material property data used is found in Table 6.2.1-5. | |||
The heat transfer coefficient to the containment structures is based primarily on the work of Tagami, Reference [21]. An explanation of the manner of application is given in Reference [3]. | |||
When applying the Tagami correlations a conservative limit was placed on the lower compartment stagnant heat transfer coefficients. They were limited to 72 Btu/hr-ft2. | |||
This corresponds to a steam-air ratio of 1.4 according to the Tagami correlation. The imposition of this limitation is to restrict the use of the Tagami correlation within the test range of steam-air ratios where the correlation was derived. | |||
6.2.1.3.4 Short-Term Blowdown Analysis TMD Code - Short-Term Analysis (1) Introduction 6.2.1-8 Containment Functional Design | |||
WATTS BAR WBNP-112 The basic performance of the ice condenser reactor containment system has been demonstrated for a wide range of conditions by the Waltz Mill Ice Condenser Test Program. These results have clearly shown the capability and reliability of the ice condenser concept to limit the Containment pressure rise subsequent to a hypothetical loss-of-coolant accident. | |||
To supplement this experimental proof of performance, a mathematical model has been developed to simulate the ice condenser pressure transients. This model, encoded as computer program TMD (Transient Mass Distribution) Reference [4], provides a means for computing pressures, temperatures, heat transfer rates, and mass flow rates as a function of time and location throughout the containment. This model is used to compute pressure differences on various structures within the containment as well as the distribution of steam flow as the air is displaced from the lower compartment. Although the TMD code can calculate the entire blowdown transient, the peak pressure differences on various structures occur within the first few seconds of the transient. | |||
(2) Analytical Models (No Entrainment) | |||
The mathematical modeling in TMD is similar to that of the SATAN blowdown code in that the analytical solution is developed by considering the conservation equations of mass, momentum and energy and the equation of state, together with the control volume technique for simulating spatial variation. The governing equations for TMD are given in Reference [4]. | |||
The moisture entrainment modifications to the TMD code are discussed, in detail, in Reference [4]. These modifications comprise incorporating the additional entrainment effects into the momentum and energy equations. | |||
As part of the review of the TMD code, additional effects are considered. | |||
Changes to the analytical model required for these studies are described in Reference [4]. | |||
These studies consist of: | |||
(a) Spatial acceleration effects in ice bed (b) Liquid entrainment in ice beds (c) Upper limit on sonic velocity (d) Variable ice bed loss coefficient (e) Variable door response (f) Wave propagation effects Additionally the TMD code has been modified to account for fluid compressibility effects in the high Mach number subsonic flow regime. | |||
Containment Functional Design 6.2.1-9 | |||
WATTS BAR WBNP-112 Experimental Verification The performance of the TMD code was verified against the 1/24 scale air tests and the 1968 Waltz Mill tests. For the 1/24 scale model the TMD code was utilized to calculate flow rates to compare against experimental results. The effect of increased nodalization was also evaluated. The Waltz Mill test comparisons involved a reexamination of test data. In conducting the reanalyses, representation of the 1968 Waltz Mill test was reviewed with regard to parameters such as loss coefficients and blowdown time history. The details of this information are given in Reference [4]. | |||
The Waltz Mill Ice Condenser Blowdown Test Facility was reactivated in 1973 to verify the ice condenser performance with the following redesigned plant hardware scaled to the test configuration: | |||
(1) Perforated metal ice baskets and new design couplings. | |||
(2) Lattice frames sized to provide the correct loss coefficient relative to plant design. | |||
(3) Lower support beamed structure and turning vanes sized to provide the correct turning loss relative to the plant design. | |||
(4) No ice baskets in the lower ice condenser plenum opposite the inlet doors. | |||
The result of these tests was to confirm that conclusions derived from previous Waltz Mill tests have not been significantly changed by the redesign of plant hardware. The TMD Code has, as a result of the 1973 test series, been modified to match ice bed heat transfer performance. Detailed information on the 1973 Waltz Mill test series is found in Reference [5]. | |||
Application to Plant Design (General Description) | |||
As described in Reference [4], the control volume technique is used to spatially represent the containment. The containment is divided into 50 elements to give a detailed representation of the local pressure transient on the containment shell and internal concrete structures. This division of the containment is similar for all ice condenser plants. | |||
The Watts Bar plant containment has been divided into 50 elements or compartments as shown in Figures 6.2.1-5, 6.2.1-6, 6.2.1-7, and 6.2.1-8. The interconnections between containment elements in the TMD code is shown schematically in Figure 6.2.1-9. Flow resistance and inertia are lumped together in the flow paths connecting the elements shown. The division of the lower compartments into 6 volumes occurs at the points of greatest flow resistance, i.e., the four steam generators, pressurizer and refueling cavity. | |||
Each of these lower compartment sections delivers flow through doors into a section behind the doors and below the ice bed. Each vertical section of the ice bed is, in turn, divided into three elements. The upper plenum between the top of the ice bed and the upper doors is represented by an element. Thus, a total of thirty elements (Elements 6.2.1-10 Containment Functional Design | |||
WATTS BAR WBNP-112 7 through 24 and 38 through 49 are used to simulate the ice condenser). The six elements at the top of the ice bed between bed and upper doors deliver to element number 25 the upper compartment. Note that cross flow in the ice bed is not accounted for in the analysis; this yields the most conservative results for the particular calculations described herein. The upper reactor cavity (Element 33) is connected to the lower compartment volumes and provides cross flow for pressure equalization of the lower compartments. The less active compartments, called dead-ended compartments (Elements 26 through 32 and 34 through 37) outside the crane wall are pressurized by ventilation openings through the crane wall into the fan compartments. | |||
For each element in the TMD network the volume, initial pressure and initial temperature conditions are specified. The ice condenser elements have additional inputs of mass of ice, heat transfer area and condensate layer length. For each flow path between elements flow resistance is specified as a loss coefficient "K" or a fraction loss "L/D" or a combination of the two based on the flow area specified between elements. Friction factor, friction factor length and hydraulic diameter are specified for the friction loss. | |||
Additionally, input for each flow path includes the area ratio (minimum area/maximum area) which is used to account for compressibility effects across flow path contractions. | |||
The code input for each flow path is the flow path length used in the momentum equation. The ice condenser loss coefficients have been based on the 1/4-scale tests representative of the current ice condenser geometry. The test loss coefficient was increased to include basket roughness effects and to include intermediate and top deck pressure losses. The loss coefficient is based on removal of door port flow restrictors. | |||
To better represent short term transients effects, the opening characteristics of the lower, intermediate, and top deck ice condenser doors have been modeled in the TMD code. The containment geometric data for the elements and flow paths used in the TMD code is confirmed to agree with the actual design by TVA and Westinghouse. An initial containment pressure of 0.3 psig was assumed in the analysis. Initial containment pressure variation about the assumed 0.3 psig value has only a slight affect on the initial pressure peak and the compression ratio pressure peak. TMD input data is given in Tables 6.2.1-6 and 6.2.1-7. | |||
The reactor coolant blowdown rates used in these cases are based on the SATAN analysis of a double-ended rupture of either a hot or a cold leg reactor coolant pipe utilizing a discharge coefficient of 1.0. The models and assumptions used to calculate the short-term mass and energy releases are described in Reference [9]. Tables 6.2.1-23 and 6.2.1-24 present the mass and energy release data used for this analysis. | |||
A number of analyses have been performed to determine the various pressure transients resulting from hot and cold leg reactor coolant pipe breaks in any one of the six lower compartment elements. The analyses were performed using the following assumptions and correlations: | |||
(1) Flow was limited by the unaugmented critical flow correlation. | |||
Containment Functional Design 6.2.1-11 | |||
6.1- | WATTS BAR WBNP-112 (2) The TMD variable volume door model, which accounts for changes in the volumes of TMD elements as the door opens, was implemented. | ||
(3) The heat transfer calculation used was based on performance during the 1973-1974 Waltz Mill test series. A higher value of the ELJAC parameter has been used and an upper bound on calculated heat transfer coefficients has been imposed[5]. | |||
(4) One hundred percent moisture entrainment was assumed. | |||
(5) Compressibility effects due to flow area contractions were modeled. | |||
Figures 6.2.1-10 and 6.2.1-11 are representative of the typical upper and lower compartment pressure transients that result from a hypothetical double-ended rupture of a reactor coolant pipe for the worst possible location in the lower compartment of the containment; i.e., hot leg and cold leg breaks in Element 1. | |||
Initial Pressures Results of the analysis for the Watts Bar Plant are presented in Tables 6.2.1-8 through 6.2.1-11. The peak pressures and peak differential pressures resulting from hot and cold leg reactor coolant pipe breaks in each of the six lower compartment control volumes were calculated. | |||
Table 6.2.1-8 presents the maximum calculated pressure peak for the lower compartment elements resulting from hot and cold leg double ended pipe breaks. | |||
Generally, the maximum peak pressure within a lower compartment element results when the pipe break occurs in that element. A cold leg break in Element 1 creates the highest pressure peak, also in Element 1, of 18.5 psig. | |||
Table 6.2.1-9 presents the maximum calculated peak pressure in each of the ice condenser sections resulting from any pipe break location. The maximum peak pressure in each of the ice condenser sections is found in the lower plenum element of the section. The peak pressure was calculated to be 13.9 psig in Element 40. | |||
Table 6.2.1-10 presents the maximum calculated differential pressures across the operating deck (divider barrier) between the lower compartment elements and the upper compartment. These values are approximately the same as the maximum calculated differential pressure across the lower crane wall between the lower compartment elements and the dead ended volumes surrounding the lower compartment. The peak differential pressure of 16.6 psi was calculated to be between Elements 1 and 25 for a cold leg break. | |||
Table 6.2.1-11 presents the maximum calculated differential pressures across the upper crane wall between the upper ice condenser elements and the upper compartment. The peak differential of 8.4 psi pressure was calculated to be between Element 7-8-9 and 25 for a hot leg pipe break. | |||
6.2.1-12 Containment Functional Design | |||
WATTS BAR WBNP-112 Consideration is given to the calculation of subcompartment pressures (and pressure differentials) for cases other than the design basis double ended reactor coolant pipe rupture in the lower compartment. Discussion of these analyses is treated in Section 6.2.1.3.9. | |||
Functional Design 6.2.1 | Sensitivity Studies A series of TMD runs for D. C. Cook investigated the sensitivity of peak pressures to variations in individual input parameters for the design basis blowdown rate and 100 percent entrainment. This analysis used a DEHL break in Element 6 of D. C. Cook. | ||
Table 6.2.1-12 presents the results of this sensitivity study. | |||
As part of the short-term containment pressure analysis of ice condenser units, the pressure response to both DEHL and DECL breaks are routinely considered for each of the loop compartments. | |||
Choked Flow Characteristics The data in Figure 6.2.1-12 illustrate the behavior of mass flow rate as a function of upstream and downstream pressures, including the effects of flow choking. The upper plot shows mass flow rate as a function of upstream pressure for various assumed values of downstream pressure. For zero back pressure (Pd = 0), the entire curve represents choked flow conditions with the flow rate approximately proportional to upstream pressure Pu. For higher back pressure, the flow rates are lower until the upstream pressure is high enough to provide choked flow. After the increase in upstream pressure is sufficient to provide flow chokings further increases in upstream pressure cause increases in mass flow rate along the curve for Pd = 0. The key point in this illustration is that flow rate continues to increase with increasing upstream pressure, even after flow choking conditions have been reached. Thus, choking does not represent a threshold beyond which dramatically sharper increases in compartment pressures could be expected because of limitations on flow relief to adjacent compartments. | |||
The phenomenon of flow choking is more frequently explained by assuming a fixed upstream pressure and examining the dependence of flow rate with respect to decreasing downstream pressure. This approach is illustrated for an assumed upstream pressure of 30 psia as shown in the upper plot with the results plotted vs. | |||
downstream pressure in the lower plot. For fixed upstream conditions, flow choking represents an upper limit flow rate beyond which further decreases in back pressure do not produce any increase in mass flow rate. | |||
Compression Ratio Analysis As blowdown continues following the initial pressure peak from a double-ended cold leg break, the pressure in the lower compartment again increases, reaching a peak at or before the end of blowdown. The pressure in the upper compartment continues to rise from beginning of blowdown and reaches a peak which is approximately equal to the lower compartment pressure. After blowdown is complete, the steam in the lower Containment Functional Design 6.2.1-13 | |||
WATTS BAR WBNP-112 compartment continues to flow through the doors into the ice bed compartment and is condensed. | |||
The primary factor in producing this upper containment pressure peak and, therefore, in determining design pressure, is the displacement of air from the lower compartment into the upper containment. The ice condenser quite effectively performs its function of condensing virtually all the steam that enters the ice beds. Essentially, the only source of steam entering the upper containment is from leakage through the drain holes and other leakage around crack openings in hatches in the operating deck separating the lower and upper portions of the containment building. | |||
A method of analysis of the compression peak pressure was developed based on the results of full-scale section tests. This method consists of the calculation of the air mass compression ratio, the polytropic exponent for the compression process, and the effect of steam bypass through the operating deck on this compression. | |||
The compression peak pressure in the upper containment for the Watts Bar plant design is calculated to be 7.81 psig (for an initial air pressure of 0.3 psig). This compression pressure includes the effect of a pressure increase of 0.4 psi from steam bypass and also for the effects of the dead-ended volumes. The nitrogen partial pressure from the accumulators is not included since this nitrogen is not added to the containment until after the compression peak pressure has been reduced, which is after blowdown is completed. This nitrogen is considered in the analysis of pressure decay following blowdown as presented in the long term performance analysis using the LOTIC code. The following sections discuss the major parameters affecting the compression peak. Specifically they are: air compression, steam bypass, blowdown rate, and blowdown energy. | |||
Air Compression Process Description The volumes of the various containment compartments determine directly the air volume compression ratio. This is basically the ratio of the total active containment air volume to the compressed air volume during blowdown. During blowdown air is displaced from the lower compartment and compressed into the ice condenser beds and into the upper containment above the operating deck. It is this air compression process which primarily determines the peak in containment pressure, following the initial blowdown release. A peak compression pressure of 7.81 psig is based on the Watts Bar Plant design compartment volumes shown in Table 6.2.1-13. | |||
Figure 6.2.1-13 shows the sensitivity of the compression peak pressure with different air compression ratios. | |||
Methods of Calculation and Results Full-Scale Section Tests The actual Waltz Mill test compression ratios were found by performing air mass balances before the blowdown and at the time of the compression peak pressure, 6.2.1-14 Containment Functional Design | |||
WATTS BAR WBNP-112 using the results of three full-scale special section tests. These three tests were conducted with an energy input representative of the plant design. | |||
In the calculation of the mass balance for the ice condenser, the compartment is divided into two sub-volumes; one volume representing the flow channels and one volume representing the ice baskets. The flow channel volume is further divided into four sub-volumes. The partial air pressure and mass in each sub-volume is found from thermocouple readings by assuming that the air is saturated with steam at the measured temperature. From these results, the average temperature of the air in the ice condenser compartment is found, and the volume occupied by the air at the total condenser pressure is found from the equation of state as follows: | |||
M a2 R a T a2 V a2 = ---------------------------- (1) | |||
P2 where: | |||
Va2 = Volume of ice condenser occupied by air (ft3) | |||
Ma2 = Mass of air in ice condenser compartment (lb) | |||
Ta2 = Average temperature of air in ice condenser (°F) | |||
P2 = Total ice condenser pressure (lb/ft2) | |||
Ra = Ideal gas constant The partial pressure and mass of air in the lower compartment are found by averaging the temperatures indicated by the thermocouples located in that compartment and assuming saturation conditions. For these three tests, it was found that the partial pressure, and hence the mass of air in the lower compartment, was zero at the time of the compression peak pressure. | |||
The actual Waltz Mill test compression ratio is then found from the following: | |||
V1 + V2 + V3 C = -------------------------------- (2) | |||
V 3 + V a2 where: | |||
V1 = Lower compartment volume (ft3) | |||
V2 = Ice condenser compartment volume (ft3) | |||
Containment Functional Design 6.2.1-15 | |||
WATTS BAR WBNP-112 V3 = Upper compartment volume (ft3) | |||
The polytropic exponent for these tests is then found from the measured compression pressure and the compression ratio calculated above. Also considered is the pressure increase that results from the leakage of steam through the deck into the upper compartment. | |||
The compression peak pressure in the upper compartment for the tests or containment design is then given by: | |||
n P = P o (Cr ) + Pdeck (3) where: | |||
Po = Initial pressure (psia) | |||
P = Compression peak pressure (psia) | |||
Cr = Volume compression ratio n = Polytropic exponent Pdeck = Pressure increase caused by deck leakage (psi) | |||
Using the method of calculation described above, the compression ratio is calculated for the three full-scale section tests. From the results of the air mass balances, it was found that air occupied 0.645 of the ice condenser compartment volume at the time of peak compression, or V a2 = 0.645 V 2 (4) | |||
The final compression volume includes the volume of the upper compartment as well as part of the volume of air in the ice condenser. The results of the full-scale section tests (Figure 6.2.1-14) show a variation in steam partial pressure from 100% near the bottom of the ice condenser to essentially zero near the top. The thermocouples and pressure detectors confirm that at the time when the compression peak pressure is reached steam occupies less than half of the volume of the ice condenser. The analytical model used in defining the containment pressure peak uses upper compartment volume plus 64.5% of the ice condenser air volumes as the final volume. | |||
This 64.5% value was determined from appropriate test results. | |||
The calculated volume compression ratios are shown in Figure 6.2.1-15, along with the compression peak pressures for these tests. The compression peak pressure is determined from the measured pressure, after accounting for the deck leakage contribution. From the results shown in Figure 6.2.1-15, the polytropic exponent for these tests is found to be 1.13. | |||
6.2.1-16 Containment Functional Design | |||
WATTS BAR WBNP-112 Plant Case For the Watts Bar design, the volume compression ratio is calculated using Equation 2, modeling the upper plenum as part of the upper compartment, and Table 6.2.1-13 as: | |||
1, 077, 012 C r = --------------------------------------------------------------------------------- (5) 692, 818 + [ 0.645 X 110, 520 ] | |||
Cr = 1.4095 The peak compression pressure, based on an initial containment pressure of 15.0 psia (0.3 psig), is then given by Equation 3 as: | |||
P3 = 15.0 (1.4095)1.13 + 0.4 P3 = 22.507 psia or 7.81 psig This peak compression pressure includes a pressure increase of 0.4 psi from steam bypass through the deck (see Section 6.2.1.3.5). | |||
Sensitivity to Blowdown Energy The sensitivity of the upper and lower compartment peak pressure versus blowdown rate as measured from the 1974 Waltz Mill Tests is shown in Figure 6.2.1-16. This figure shows the magnitude of the peak pressure versus the amount of energy released in terms of percentage of RCS energy release rate. | |||
Percent energy blowdown rate was selected for the plot because energy flow rate more directly relates to volume flow rate and therefore pressure. There are two important effects to note from the peak upper compartment pressure versus blowdown rate: | |||
(1) the magnitude of the final peak pressure in the upper compartment is low (about 9 psig) for the plant design DECL blowdown rate; (2) even an increase in this rate up to 141% of the blowdown energy rate produces only a small increase in the magnitude of this peak pressure (about 1 psi). The major factor setting the peak pressure reached in the upper compartment is the compression of air displaced by steam from the lower compartment into the upper compartment. The lower compartment initial peak pressure shows a relatively low peak pressure of 12.9 psig for the design basis DECL blowdown rate, and even a substantial increase in blowdown energy rate (141% | |||
reference initial DECL) would cause an increase in initial peak pressure of only 3 psi. | |||
The peak pressure in the lower compartment is due mainly to flow resistance caused by displacement of air from the lower compartment into the upper compartment. | |||
6.2.1.3.5 Effect of Steam Bypass The sensitivity of the compression peak pressure to deck bypass is shown in Figure 6.2.1-17, which shows that an increase in deck bypass area of 50% would cause an increase of about 0.2 psi in final peak compression pressure. Also, it is important to note that the plant final peak compression pressure of 7.81 psig already includes a contribution of 0.4 psi from the plant deck bypass area of 5 ft2. | |||
Containment Functional Design 6.2.1-17 | |||
WATTS BAR WBNP-112 This effect of deck leakage on upper containment pressure has been verified by a series of four special, full-scale section tests. These tests were all identical except different size deck leakage areas were used. | |||
The results of these tests are given in Figure 6.2.1-18 which includes two curves of test results. Each curve shows the difference in upper compartment pressure between one test and another resulting from a difference in deck leakage area. One curve shows the increase in upper compartment pressure at the end of the boiler blowdown (after the compression peak pressure, at about 50 seconds in these tests), and the second curve shows the increase in upper compartment peak pressure (at about 10 seconds in these tests). It should be noted that the pressure at the end of the blowdown is less than the peak compression ratio pressure occurring at about 10 seconds for reference blowdown test. | |||
The containment pressure increase due to deck leakage is directly proportional to the total amount of steam leakage into the upper compartment, and the amount of this steam leakage is, in turn, proportional to the amount of steam released from the boiler, less the inventory of steam remaining in the lower compartment. Notably, the increase in upper compartment compression peak pressure is substantially less than the upper compartment pressure increase at the end of blowdown, because the peak compression pressure occurs before the boiler has released all of its energy. | |||
The calculated maximum pressure rise due to deck leakage (when all of the boiler energy release has occurred) is also shown in Figure 6.2.1-18. The slope of this curve is 0.095 psi/ft2 for the tests and is equivalent to 0.107 psi/ft2 for the plant design. The difference between the two coefficients is due to a small difference in upper compartment volume between the plant design and these tests. | |||
As shown in Figure 6.2.1-18, the calculated curve for maximum pressure increase at the end of blowdown agrees closely with the measured curve at small deck leakage areas but deviates at larger leakage areas. This deviation apparently results from the condensation of upper compartment steam by the walls of the upper compartment and by the ice at the top of the condenser during the tests. Pressure would also be reduced by heat losses in a plant; however, for conservatism, no credit is taken for this effect. | |||
As demonstrated by tests, the compression peak pressure in the upper compartment occurs before the boiler releases all of its energy, and the measured increase in peak compression pressure due to increased deck leakage, is proportionately reduced. For the case of the plant design, the final peak compression pressure is conservatively assumed to occur when the reactor coolant system release is 75% of its total energy. | |||
This value is selected as a reference value, based on the results of a number of tests conducted with different blowdown rates and total energy releases, as shown in Figure 6.2.1-19. The actual deck leakage coefficient is therefore: | |||
P 3 | |||
- = 0.107 x 0.75 = 0.080psi/ft 2 A deck 6.2.1-18 Containment Functional Design | |||
flow.In conclusion, it is apparent that there is a substantial margin between the design deck leakage area of 5 | WATTS BAR WBNP-112 The divider barrier including the enclosures over the pressurizer, steam generators and reactor vessel, is designed to provide a reasonably tight seal against leakage. | ||
6.2.1.3.6 | Holes are purposely provided in the bottom of the refueling cavity to allow water from sprays in the upper compartment to drain to the sump in the lower compartment. | ||
6.2.1- | Potential leakage paths exist at all the joints between the operating deck and the pump access hatches and reactor vessel enclosure slabs. The total of all deck leakage flow areas is approximately 5 ft2. The effect of this potential leakage path is small and is found to be: | ||
After the broken loop steam generator cools, the break flow becomes two phase.Break Size and Location Generic studies have been performed with respect to the effect of postulated break size on the LOCA mass and energy releases. The double-ended guillotine break has been found to be limiting due to larger mass flow rates during the blowdown phase of the transient. During the reflood and froth phases, the break size has little effect on the releases.Three distinct locations in the RCS loop can be postulated for pipe rupture:1. Hot leg (between vessel and steam generator)2. Cold leg (between pump and vessel) | Pdeck = 5 x 0.080 = 0.4 psi In the event that the reactor coolant system break flow is so small that it would leak through these flow paths without developing sufficient differential pressure (1 lb/ft2) to open the ice condenser doors, steam from the break would slowly pressurize the containment. The containment spray system has sufficient capacity to maintain pressure well below design for this case. | ||
The Watts Bar Nuclear Plant and the Sequoyah Nuclear Plant are geometrically very similar. Some differences between the two plants, are the design pressure, spray flow rates, and a slight difference in thermal ratings. The fact that the spray flow rate is higher for the Sequoyah plant (4750 gpm versus 4000 gpm) is offset by Watts Bar's higher maximum internal pressure (15 psig versus 12 psig). The following discussion presents the deck leakage analysis performed for the Sequoyah plant. The purpose of this analysis is only to show the substantial margin which exists between the design deck leakage of 5 ft2 and the tolerable deck leakage. The Sequoyah analysis which shows conservatism by a factor of 7, is more than sufficient for this purpose. | |||
The method of analysis used to obtain the maximum allowable deck leakage capacity as a function of the primary system break size is as follows. | |||
During the blowdown transient, steam and air flow through the ice condenser doors and also through the deck bypass area into the upper compartment. For the containment, this bypass area is composed of two parts, a known leakage area of 2.2 ft2 with a geometric loss coefficient of 1.5 through the deck drainage holes location at the bottom of the refueling canal and an undefined deck leakage area with a conservatively small loss coefficient of 2.5. | |||
A resistance network similar to that used to TMD is used to represent 6 lower compartment volumes each with a representative portion of the deck leakage, and the lower inlet door flow resistance and flow area is calculated for small breaks that would only partially open these doors. The coolant blowdown rate as a function of time is used with this flow network to calculate the differential pressures on the lower inlet doors and across the operating deck. | |||
The resultant deck leakage rate and integrated steam leakage into the upper compartment is then calculated. The lower inlet doors are initially held shut by the cold head of air behind the doors (approximately one pound per square foot). The initial blowdown from a small break opens the doors and removes the cold head on the doors. With the door differential removed, the door position is slightly open. An Containment Functional Design 6.2.1-19 | |||
WATTS BAR WBNP-112 additional pressure differential of one pound per square foot is then sufficient to fully open the doors. The nominal door opening characteristics are based on test results. | |||
One analysis conservatively assumed that flow through the postulated leakage paths is pure steam. During the actual blowdown transient, steam and air representative of the lower compartment mixture leak through the holes, thus less steam would enter the upper compartment. If flow were considered to be a mixture of liquid and vapor, the total leakage mass would increase, but the steam flow rate would decrease. The analysis also assumed that no condensing of the flow occurs due to structural heat sinks. The peak air compression in the upper compartment for the various break sizes is assumed with steam mass added to this value to obtain the total containment pressure. Air compression for the various break sizes is obtained from previous full-scale section tests conducted at Waltz Mill. | |||
The allowable leakage area for the following reactor coolant system (RCS) break sizes was determined: DE, 0.6 DE, 3 ft2, 10 inch diameter, 6 inch diameter, 2 inch diameter, and 0.5 inch diameter. The allowable deck leakage area for the DE break was based on the test results previously discussed. For break sizes of 3 ft2 and 0.6 DE, a series of deck leakage sensitivity studies were made to establish the total steam leakage to the upper compartment over the blowdown transient. This steam was added to the peak compression air mass in the upper compartment to calculate a peak pressure. | |||
Air and steam were assumed to be in thermal equilibrium, with the air partial pressure increased over the air compression value to account for heating effects. For these breaks, sprays were neglected. Reduction in compression ratio by return of air to the lower compartment was conservatively neglected. The results of this analysis are shown in Table 6.2.1-14. This analysis is confirmed by Waltz Mill tests conducted with various deck leaks equivalent to over 50 ft2 feet of deck leakage for the double-ended blowdown rate and is shown in Figure 6.2.1-20. | |||
For breaks of 10 inch diameter and smaller, the effect of containment sprays was included. The method used calculates, for each time step of the blowdown, the amount of steam leaking into the upper compartment to obtain the steam mass in the upper compartment. This steam was mixed with the air in the upper compartment, assuming thermal equilibrium with air. The air partial pressure was increased to account for air heating effects. After sprays were initiated, the pressure was calculated based on the rate of accumulation of steam in the upper compartment. | |||
This analysis was conducted for the 10 inch, 6 inch, and 2 inch break sizes, assuming one spray pump operated (4750 gpm at 100°F). As shown in Table 6.2.1-14, the 10 inch break is the limiting case for the given range of break sizes. | |||
A second, more realistic, method was used to analyze the 10 inch, 6 inch, and 2 inch breaks. This analysis assumed a 30% air and 70% steam mix flowing through the deck leakage area. This is conservative considering the amount of air in the lower compartment during this portion of the transient. Operation of the deck fan increases the air content of the lower compartment, thus increasing the allowable deck leakage area. Based on the LOTIC code analysis, a structural heat removal rate of over 6000 Btu/sec from the upper compartment is indicated. Therefore, a steam condensation 6.2.1-20 Containment Functional Design | |||
WATTS BAR WBNP-112 rate of 6 lbs/sec was used for the upper compartment. The results indicate that with one spray pump operating and a deck leakage area of 50 ft2, the peak containment pressure is below design pressure. | |||
The 1/2 inch diameter break is not sufficient to open the ice condenser inlet doors. For this break, the upper compartment spray is sufficient to condense the break steam flow. | |||
In conclusion, it is apparent that there is a substantial margin between the design deck leakage area of 5 ft2 and that which can be tolerated without exceeding containment design pressure. A preoperational visual inspection is performed to ensure that the seals between the upper and lower containment have been properly installed. | |||
6.2.1.3.6 Mass and Energy Release Data Long-Term Loss-of-Coolant Accident Mass and Energy Releases The evaluation model used for the long-term LOCA mass and energy release calculations is the March 1979 model described in Reference 20. This evaluation model has been reviewed and approved by the NRC. | |||
The time history of conditions within an ice condenser containment during a postulated loss-of-coolant accident (LOCA) can be divided into two periods: | |||
: 1. The initial reactor coolant blowdown, which for the largest assumed pipe break occurs within approximately 30 seconds. | |||
: 2. The post blowdown phase of the accident which begins following the blowdown and extends several hours after the start of the accident. | |||
LOCA Mass and Energy Release Phases The containment system receives mass and energy releases following a postulated rupture in the RCS. These releases continue over a time period, the LOCA analysis calculational model is typically divided into four phases: | |||
: 1. Blowdown - the period of time from accident initiation (when the reactor is at steady-state operation) to the time that the RCS and containment reach an equilibrium state at containment design pressure. | |||
: 2. Refill - the period of time when the reactor vessel lower plenum is being filled by accumulator and Emergency Core Cooling System (ECCS) water. At the end of blowdown, a large amount of water remains in the cold legs, downcomer, and lower plenum. To conservatively consider the refill period for the purpose of containment mass and energy releases, it is assumed that this water is instantaneously transferred to the lower plenum along with sufficient accumulator water to completely fill the lower plenum. This allows an uninterrupted release of mass and energy to containment. Therefore, the refill period is conservatively neglected in the mass and energy release calculation. | |||
Containment Functional Design 6.2.1-21 | |||
WATTS BAR WBNP-112 | |||
: 3. Reflood - begins when the water from the reactor vessel lower plenum enters the core and ends when the core is completely quenched. | |||
: 4. Post-reflood (Froth) - describes the period following the reflood transient. For the pump suction break, a two-phase mixture exits the core, passes through the hot legs, and is superheated in the steam generators prior to release to containment. | |||
After the broken loop steam generator cools, the break flow becomes two phase. | |||
Break Size and Location Generic studies have been performed with respect to the effect of postulated break size on the LOCA mass and energy releases. The double-ended guillotine break has been found to be limiting due to larger mass flow rates during the blowdown phase of the transient. During the reflood and froth phases, the break size has little effect on the releases. | |||
Three distinct locations in the RCS loop can be postulated for pipe rupture: | |||
: 1. Hot leg (between vessel and steam generator) | |||
: 2. Cold leg (between pump and vessel) | |||
: 3. Pump suction (between steam generator and pump) | : 3. Pump suction (between steam generator and pump) | ||
For long-term considerations the break location analyzed is the pump suction double-ended guillotine (DEPSG) (10.46 | For long-term considerations the break location analyzed is the pump suction double-ended guillotine (DEPSG) (10.46 ft2). The pump suction break mass and energy releases have been calculated for the blowdown, reflood, and post-reflood phases of the LOCA for each case analyzed. The following paragraphs provide a discussion on each break location. | ||
The hot-leg double-ended guillotine has been shown in previous studies to result in the highest blowdown mass and energy release rates. Although the core flooding rate would be the highest for this break location, the amount of energy released from the steam generator secondary is minimal because the majority of the fluid that exits the core bypasses the steam generators, venting directly to containment. As a result, the reflood mass and energy releases are reduced significantly as compared to either the pump suction or cold-leg break locations, where the core exit mixture must pass through the steam generators before venting through the break. | |||
For the hot-leg break, generic studies have confirmed that there is no reflood peak (that is, from the end of the blowdown period the containment pressure would continually decrease). The mass and energy releases for the hot-leg break have not been included in the scope of this containment integrity analysis because, for the hot-leg break, only the blowdown phase of the transient is of any signifcance. Since there are no reflood or post-reflood phases to consider, the limiting peak pressure calculated would be the compression peak pressure and not the peak pressure following ice bed melt-out. | |||
The cold-leg break location has been found in previous studies to be much less limiting in terms of the overall containment energy releases. The cold-leg blowdown is faster 6.2.1-22 Containment Functional Design | |||
WATTS BAR WBNP-112 than that of the pump suction break, and more mass is released into the containment. | |||
However, the core heat transfer is greatly reduced, and this results in a considerably lower energy release into containment. Studies have determined that the blowdown transient for the cold leg is less limiting than that tor the pump suction break. During cold-leg reflood, the flooding rate is greatly reduced and the energy release rate into the containment is reduced. Therefore, the cold-leg break is not included in the scope of this analysis. | |||
The pump suction break combines the effects of the relatively high core flooding rate, as in the hot-leg break, and the addition of the stored energy in the steam generators. | |||
As a result, the pump suction break yields the highest energy flow rates during the post-blowdown period by including all of the available energy of the RCS in calculating the releases to containment. This break has been determined to be the limiting break for all ice condenser plants. | |||
In summary, the analysis of the limiting break location for an ice condenser containment has been performed. The DEPSG break has historically been considered to be the limiting break location, by virtue of its consideration of alI energy sources in the RCS. This break location provides a mechanism for the release of the available energy in the RCS, including both the broken and intact loop steam generators. | |||
Inclusion of these energy sources conservatively results in the maximum amount of ice being melted in the event of a LOCA. | |||
Application of Single-Failure Criteria An analysis of the effects of the single-failure criteria has been performed on the mass and energy release rates for the pump suction (DEPSG) break. An inherent assumption in the generation of the mass and energy release is that offsite power is lost. This results in the actuation of the emergency diesel generators, required to power the Safety Injection System. This is not an issue for the blowdown period, which is limited by the compression peak pressure. | |||
The limiting minimum safety injection case has been analyzed for the effects of a single failure. In the case of minimum safeguards, the single failure postulated to occur is the loss of an emergency diesel generator. This results in the loss of one pumped safety injection train, that is, ECCS pumps and heat exchangers. | |||
Basis of the Analysis I. Significant Modeling Assumptions The following summarized assumptions were employed to ensure that the mass and energy releases were conservatively calculated, thereby maximizing energy release to containment: | |||
: 1. Maximum expected operating temperature of the RCS at 100-percent full-power conditions: (619.1°F) | |||
Containment Functional Design 6.2.1-23 | |||
WATTS BAR WBNP-112 | |||
: 2. An alIowance in temperature for instrument error and dead band was assumed on the vessel/core inlet temperature (+7.0°F) | |||
: 3. Margin in volume of 3 percent (which is composed of a 1.6-percent allowance for thermal expansion, and a 1.4-percent alIowance for uncertainty) | |||
: 4. Core rated power of 3,411 MWt | |||
: 5. Allowance for calorimetric error (+2.0 percent of power) | : 5. Allowance for calorimetric error (+2.0 percent of power) | ||
: 6. Conservative coefficient of heat transfer (that is, steam generator primary/secondary heat transfer and RCS metal heat transfer).7. Core-stored energy based on the time in life for maximum fuel densification. The assumptions used to calculate the fuel temperatures for the core-stored energy calculation account for appropriate uncertainties associated with the models in the PAD code (such as calibration of the thermal model, pellet densification model, or clad creep model). In addition, the fuel temperatures for the core-stored energy calculation account for appropriate uncertainties associated with manufacturing tolerances (such as pellet as-built density). The total uncertainty for the fuel temperature calculation is a statistical combination of these effects and is dependent upon fuel type, power level, and burnup.8. An allowance for RCS initial pressure uncertainty (+70 psi) | : 6. Conservative coefficient of heat transfer (that is, steam generator primary/secondary heat transfer and RCS metal heat transfer). | ||
: 7. Core-stored energy based on the time in life for maximum fuel densification. The assumptions used to calculate the fuel temperatures for the core-stored energy calculation account for appropriate uncertainties associated with the models in the PAD code (such as calibration of the thermal model, pellet densification model, or clad creep model). In addition, the fuel temperatures for the core-stored energy calculation account for appropriate uncertainties associated with manufacturing tolerances (such as pellet as-built density). The total uncertainty for the fuel temperature calculation is a statistical combination of these effects and is dependent upon fuel type, power level, and burnup. | |||
: 8. An allowance for RCS initial pressure uncertainty (+70 psi) | |||
: 9. A maximum containment backpressure equal to design pressure | : 9. A maximum containment backpressure equal to design pressure | ||
: 10. A provision for modeling steam flow in the secondary side through the steam generator turbine stop valve was conservatively addressed only at the start of the event. A turbine stop valve isolation time equal to 0.0 seconds was used.11. As noted in Section 2.4 of Reference 20, the option to provide more specific modeling pertaining to decay heat has been exercised to specifically reflect the Watts Bar Nuclear Plant Unit 2 core heat generation, while retaining the two sigma uncertainty to assure conservatism.12. Steam generator tube plugging leveling (0-percent uniform)a. Maximizes reactor coolant volume and fluid release | : 10. A provision for modeling steam flow in the secondary side through the steam generator turbine stop valve was conservatively addressed only at the start of the event. A turbine stop valve isolation time equal to 0.0 seconds was used. | ||
: 11. As noted in Section 2.4 of Reference 20, the option to provide more specific modeling pertaining to decay heat has been exercised to specifically reflect the Watts Bar Nuclear Plant Unit 2 core heat generation, while retaining the two sigma uncertainty to assure conservatism. | |||
: 12. Steam generator tube plugging leveling (0-percent uniform) | |||
: a. Maximizes reactor coolant volume and fluid release | |||
: b. Maximizes heat transfer area across the steam generators tubes | : b. Maximizes heat transfer area across the steam generators tubes | ||
: c. Reduces coolant loop resistance, which reduces the p upstream of the break and increases break flow | : c. Reduces coolant loop resistance, which reduces the p upstream of the break and increases break flow 6.2.1-24 Containment Functional Design | ||
Containment Functional Design | |||
WATTS BAR WBNP-112 II. Initial Conditions Table 6.2.1-15 presents the System Parameters Initial Conditions utilized. | |||
Thus, based on the previously noted conditions and assumptions, a bounding analysis of Watts Bar Nuclear Plant Unit 2 is made for the release of mass and energy from the RCS in the event of a LOCA. | |||
Blowdown Mass and Energy Release Data A version of the SATAN-VI code is used for computing the blowdown transient, which is the code used for the ECCS calculation in Reference 22. The SATAN-VI code calculates blowdown (the first portion of the thermal-hydraulic transient following break initiation), including pressure, enthalpy, density, mass, energy flow rates, and energy transfer between primary and secondary systems as a function of time. | |||
The code utilizes the control volume (element) approach with the capability for modeling a large variety of thermal fluid system configurations. The fluid properties are considered uniform and thermodynamic equilibrium is assumed in each element. A point kinetics model is used with weighted feedback effects. The major feedback effects include moderator density, moderator temperature, and Doppler broadening. A critical flow calculation for subcooled (modified Zaloudek), two-phase (Moody), or superheated break flow is incorporated into the analysis. The methodology for the use of this model is described in Reference 20. | |||
Table 6.2.1-16 presents the calculated LOCA mass and energy releases for the blowdown phase of the DEPSG break. For the pump suction breaks, break path 1 in the mass and energy release tables refers to the mass and energy exiting from the steam generator side of the break; break path 2 refers to the mass and energy exiting from the pump side of the break. | |||
Reflood Mass and Energy Release Data The WREFLOOD code used for computing the reflood transient is a modified version of that used in the 1981 ECCS evaluation model, Reference 22. The WREFLOOD code addresses the portion of the LOCA transient where the core reflooding phase occurs after the primary coolant system has depressurized (blowdown) due to the loss of water through the break and when water supplied by the emergency core cooling refills the reactor vessel and provides cooling to the core. The most important feature is the steam/water mixing model. | |||
The WREFLOOD code consists of two basic hydraulic models - one for the contents of the reactor vessel and one for the coolant loops. The two models are coupled through the interchange of the boundary conditions applied at the vessel outlet nozzles and at the top of the downcomer. Additional transient phenomena, such as pumped safety injection and accumulators, reactor coolant pump performance, and steam generator release are included as auxiliary equations that interact with the basic models as required. The WREFLOOD code permits the capability to calculate variations (during the core reflooding transient) of basic parameters such as core Containment Functional Design 6.2.1-25 | |||
WATTS BAR WBNP-112 flooding rate, core and downcomer water levels, fluid thermodynamic conditions (pressure, enthalpy, density) throughout the primary system, and mass flow rates through the primary system. The code permits hydraulic modeling of the two flow paths available for discharging steam and entrained water from the core to the break; that is, the path through the broken loop and the path through the unbroken loops. | |||
A complete thermal equilibrium mixing condition for the steam and emergency core cooling injection water during the reflood phase has been assumed for each loop receiving ECCS water. This is consistent with the usage and application of the Reference 4 mass and energy release evaluation model. Even though the Reference 20 model credits steam/mixing only in the intact loop and not in the broken loop, justification, applicability, and NRC approval for using the mixing model in the broken loop has been documented (Reference 23). This assumption is justified and supported by test data, and is summarized as follows. | |||
The model assumes a complete mixing condition (that is, thermal equilibrium) for the steam/water interaction. The complete mixing process is made up of two distinct physical processes. The first is a two-phase interaction with condensation of steam by cold ECCS water. The second is a single-phase mixing of condensate and ECCS water. Since the steam release is the most important influence to the containment pressure transient, the steam condensation part of the mixing process is the only part that need be considered. (Any spillage directly heats only the sump.) | |||
The most applicable steam/water mixing test data has been reviewed for validation of the containment integrity reflood steam/water mixing model. This data is generated in 1/3 scale tests (Reference 24), which are the largest scale data available and thus most clearly simulate the flow regimes and gravitational effects that would occur in a pressurized water reactor (PWR). These tests were designed specifcally to study the steam/water interaction for PWR reflood conditions. | |||
From the entire series of 1/3 scale tests, one group corresponds almost directly to containment integrity reflood conditions. The injection flow rates from this group cover all phases and mixing conditions calculated during the reflood transient. The data from these tests were reviewed and discussed in detail in Reference 20. For all of these tests, the data clearly indicate the occurrence of very effective mixing with rapid steam condensation. The mixing model used in the containment integrity reflood calculation is therefore wholly supported by the 1/3 scale steam/water mixing data. | |||
Additionally, the following justification is also noted. The post-blowdown limiting break for the containment integrity peak pressure analysis is the DEPSG break. For this break, there are two flow paths available in the RCS by which mass and energy may be released to containment. One is through the outlet of the steam generator, the other is via reverse flow through the reactor coolant pump. Steam that is not condensed by ECCS injection in the intact RCS loops passes around the downcomer and through the broken loop cold leg and pump in venting to containment. This steam also encounters ECCS injection water as it passes through the broken loop cold leg, complete mixing occurs and a portion of it is condensed. It is this portion of steam, which is condensed, for which this analysis takes credit. This assumption is justified based upon the 6.2.1-26 Containment Functional Design | |||
WATTS BAR WBNP-112 postulated break location and the actual physical presence of the ECCS injection nozzle. A description of the test and test results is contained in References 20 and 24. | |||
Table 6.2.1-17 presents the calculated mass and energy release for the reflood phase of the pump suction double ended rupture with minimum safety injection. | |||
The transients of the principal parameters during reflood are given in Table 6.2.1-18. | |||
Post-Reflood Mass and Energy Release Data The FROTH code (Reference 9) is used for computing the post-reflood transient. The FROTH code is used for the steam generator heat addition calculation from the broken and intact loop steam generators. | |||
The FROTH code calculates the heat release rates resulting from a two-phase mixture level present in the steam generator tubes. The mass and energy releases that occur during this phase are typically superheated due to the depressurization and equilibration of the broken loop and intact loop steam generators. During this phase of the transient, the RCS has equilibrated with the containment pressure, but the steam generators contain a secondary inventory at an enthalpy that is much higher than the primary side. Therefore, a significant amount of reverse heat transfer occurs. Steam is produced in the core due to core decay heat. For a pump suction break, a two-phase fluid exits the core, flows through the hot legs, and becomes superheated as it passes through the steam generator. Once the broken loop cools, the break flow becomes two-phase. The methodology for the use of this model is described in Reference 20. | |||
The EPITOME code continues the FROTH post-reflood portion of the transient from the time at which the secondary side equilibrates to containment design pressure to the end of the transient. It also compiles a summary of data on the entire transient, including formal instantaneous mass and energy release tables and mass and energy balance tables with data at critical times. | |||
After steam generator depressurization/equilibration, the mass and energy release available to containment is generated directly from core boiloff/decay heat. At this time the flow split is assumed to be 100%. | |||
Table 6.2.1-19 presents the two-phase post-reflood (froth) mass and energy release data for the pump suction double-ended break case. | |||
Steam Generator Equilibration and Depressurization Steam generator equilibration and depressurization is the process by which secondary side energy is removed from the steam generators in stages. The FROTH computer code calculates the heat removal from the secondary mass until the secondary temperature is saturated at the containment design pressure. After the FROTH calculations, steam generator secondary energy is removed until the steam generator reaches Tsat at the user-specified intermediate equilibration pressure, when the secondary pressure is assumed to reach the actual containment pressure. The heat Containment Functional Design 6.2.1-27 | |||
WATTS BAR WBNP-112 removal of the broken loop steam generator and intact loop steam generators are calculated separately. | |||
During the FROTH calculations, steam generator heat removal rates are calculated using the secondary side temperature, primary side temperature, and a secondary side heat transfer coefficient determined using a modified McAdam's correlation (Reference 26). Steam generator energy is removed during the FROTH transient until the secondary side temperature reaches saturation temperature at the containment design pressure. The constant heat removal rate used is based on the final heat removal rate calculated by FROTH. The remaining steam generator energy available to be released is determined by calculating the difference in secondary energy available at the containment design pressure and that at the (lower) user-specifed equilibration pressure, assuming saturated conditions. This energy is then divided by the energy removal rate, resulting in an equilibration time. | |||
Decay Heat Model ANS Standard 5.1 (Reference 25) was used in the LOCA mass and energy release model for Watts Bar Unit 1 for the determination of decay heat energy. This standard was balloted by the Nuclear Power Plant Standards Committee (NUPPSCO) in October 1978 and subsequently approved. The official standard (Reference 25) was issued in August 1979. | |||
The primary assumptions that make this calculation specifc for the Watts Bar Nuclear Plant Unit 2 are the enrichment factor, minimum/maximum new fuel loading per cycle, and a conservative end of cycle core average burnup. A conservative lower bound for enrichment of 3 percent was used. Table 6.2.1-20 lists the decay heat curve used. | |||
Significant assumptions in the generation of the decay heat curve are the following: | |||
: 1. Decay heat sources considered are fission product decay and heavy element decay of U-239 and Np-239. | |||
: 2. Decay heat power from the following fissioning isotopes are included; U-238, U-235, and Pu-239. | |||
: 3. Fission rate is constant over the operating history of maximum power level. | |||
: 4. The factor accounting for neutron capture in fission products has been taken from Equation 11, of Reference 25 (up to 10,000 seconds) and Table 10 of Reference 25 (beyond 10,000 seconds). | |||
: 5. The fuel has been assumed to be at full power for 1,096 days. | |||
: 6. The number of atoms of U-239 produced per second has been assumed to be equal to 70 percent of the fssion rate. | |||
: 7. The total recoverable energy associated with one fission has been assumed to be 200 MeV/fssion. | |||
6.2.1-28 Containment Functional Design | |||
WATTS BAR WBNP-112 | |||
: 8. Two sigma uncertainty (two times the standard deviation) has been applied to the fission product decay. | |||
Short-Term Mass and Energy Releases The short-term mass and energy release models and assumptions are described in Reference [9]. The LOCA short-term mass and energy release data used to perform the containment analysis given in Sections 6.2.1.3.4 and 6.2.1.3.9 are listed below: | |||
Section Break Size and Location Table 6.2.1.3.4 Double-Ended Cold Leg 6.2.1-23 Guillotine Break Outside the Biological Shield 6.2.1.3.4 Double-Ended Hot Leg 6.2.1-24 Guillotine Break Outside the Biological Shield 6.2.1.3.9 Double-Ended Pressurizer 6.2.1-28 Spray Line Break 6.2.1.3.9 127 in2 Cold Leg Break at the 6.2.1-30 Reactor Vessel 6.2.1.3.7 Accident Chronology For a double-ended pump suction loss-of-coolant accident, the major events and their time of occurrence are shown in Table 6.2.1-25 for the minimum safeguards case. | |||
6.2.1.3.8 Mass and Energy Balance Tables Sources of Mass and Energy The sources of mass considered in the LOCA mass and energy release analysis are given in Table 6.2.1-26a. These sources are the RCS, accumulators, and pumped safety injection. | |||
The energy inventories considered in the LOCA mass and energy release analysis are given in Table 6.2.1-26b. The energy sources include: | |||
RCS water Accumulator water Pumped injection water Decay heat Core-stored energy RCS metal - Primary metal (includes steam generator tubes) | |||
Containment Functional Design 6.2.1-29 | |||
WATTS BAR WBNP-112 Steam generator metal (includes transition cone, shell, wrapper, and other internals) | |||
Steam generator secondary energy (includes fluid mass and steam mass) | |||
Secondary transfer of energy (feedwater into and steam out of the steam generator secondary) | |||
It should be noted that the inconsistency in the energy balance tables from the end of reflood to the time of intact loop steam generator depressurization/equilibration ("Total Available" data versus "Total Accountable") resulted from the exclusion of the reactor upper head in the analysis following blowdown. It has been concluded that the results are more conservative when the upper head is neglected. This does not affect the instantaneous mass and energy releases or the integrated values, but causes an increase in the total accountable energy within the energy balance table. | |||
The mass and energy inventories are presented at the following times, as appropriate: | |||
Time zero (initial conditions) | |||
End of blowdown time End of refill time End of reflood time Time of broken loop steam generator equilibration to pressure setpoint Time of intact loop steam generator equilibration to pressure setpoint The chronology of events for the DEPS case is shown in Table 6.2.1-25. | |||
The energy release from the zirc-water reaction is considered as part of the WCAP-1 0325-P-A (Reference 20) methodology. Based on the way that the energy in the fuel is conservatively released to the vessel fluid, the fuel cladding temperature does not increase to the point where the zirc-water reaction is significant. This is in contrast to the 10 CFR 50.46 analyses, which are biased to calculate high fuel rod cladding temperatures and therefore a non-significant zirc-water reaction. | |||
For the LOCA mass and energy calculation, the energy created by the zirc-water reaction value is small and is not explicitly provided in the energy balance tables. The energy that is determined is part of the mass and energy releases and is therefore already included in the LOCA mass and energy release. | |||
The methods and assumptions used to release various energy sources are given in Reference 20. | |||
The consideration of the various energy sources in the mass and energy release analysis provides assurance that all available sources of energy have been included 6.2.1-30 Containment Functional Design | |||
WATTS BAR WBNP-112 in this analysis. Therefore, the review guidelines presented in Standard Review Plan Section 6.2.1.3 have been satisfied. | |||
6.2.1.3.9 Containment Pressure Differentials Consideration is given in the design of the containment internal structures to localized pressure pulses that could occur following a loss-of-coolant accident or a main steam line break. If either type of pipe rupture were to occur in these relatively small volumes, the pressure would build up at a rate faster than the overall containment, thus imposing a differential pressure across the walls of the structures. | |||
These subcompartments include the steam generator enclosure, pressurizer enclosure, and upper and lower reactor cavity. Each compartment is designed for the largest blowdown flow resulting from the severance of the largest connecting pipe within the enclosure or the blowdown flow into the enclosure from a break in an adjacent region. | |||
The following paragraphs summarize the design basis calculations: | |||
Steam Generator Enclosure The worst break possible in the steam generator enclosure is a double-ended rupture of the steamline pipe at no load conditions. Based on an investigation of postulated break locations, the rupture is assumed to occur at the point where the steamline exits the steam generator. The blowdown for this break is given in Table 6.2.1-27a. The TMD computer code (Reference 4) using the compressibility factor and assuming unaugmented critical flow is used to calculate the short-term pressure transient. The nodalization of the steam generator enclosure where the break occurs is shown in Figure 6.2.1-81. Node 51 is the break element and has a flow path to the adjacent steam generator enclosure which is a mirror image of the enclosure where the break occurs. Both enclosures are nodalized in the same manner; their nodal network is shown in Figure 6.2.1-82 and their input data is given in Tables 6.2.1-27b and 6.2.1-27c. This input data assumes that the insulation remains intact. The loss coefficients were computed using Reference [12]. The maximum number of nodes used is based on the geometry of the system. The steam generator compartment is essentially symmetrical with no major obstructions to flow which would introduce asymmetric pressures. In addition, the flow path to the adjacent steam generator is at the top of the enclosure. Therefore, a significant differential pressure will not occur across the steam generator vessel. The balance of plant data is similar to that presented in Section 6.2.1.3.4. | |||
The peak pressure differentials across the steam generator enclosure, the steam generator vessel, and the steam generator separator wall are given in Table 6.2.1-27d. | |||
Figure 6.2.1-83 shows the differential pressure transient between the break element and the upper compartment (Node 25). Figures 6.2.1-84 and 6.2.1-85 illustrate the differential pressure transient across the steam generator vessel. As Figures 6.2.1-84 and 6.2.1-85 show, the pressure differentials across the vessel are low and are due solely to inertial effects. The pressure vs time curve for the break element is given in Containment Functional Design 6.2.1-31 | |||
WATTS BAR WBNP-112 Figure 6.2.1-86 and for the upper compartment (Node 25) in Figure 6.2.1-86a (Refer to Section 3.8.3.4.8 for steam generator compartment structural design description). | |||
Pressurizer Enclosure The worst break possible in the pressurizer enclosure is a double-ended rupture of the six-inch spray line. The rupture is assumed to occur at the top of the enclosure. The blowdown for this break is given in Table 6.2.1-28. The TMD computer code using the compressibility factor and assuming unaugmented critical flow is used to calculate the short-term pressure transient. The nodalization of the enclosure is shown in Figure 6.2.1-87. Node 51 is the break element. The input data is given in Table 6.2.1-29a. | |||
This input data assumes that the insulation remains intact. The loss coefficients were computed using Reference [12]. The maximum number of nodes used was based on the geometry of the system. The pressurizer compartment is essentially symmetrical with no major obstructions to flow which would introduce asymmetric pressures on the pressurizer vessel. The balance of plant data is similar to that presented in Section 6.2.1.3.4. | |||
The peak pressure differentials across the pressurizer enclosure's walls, and across the pressurizer vessel are given in Table 6.2.1-29b. Figure 6.2.1-88 shows the pressure transient between the break element and the upper compartment (Node 25). | |||
As Figures 6.2.1-89 through 6.2.1-91 show, the significant pressure differential across the vessel are low, occur early, and are due solely to inertial effects. The pressure vs. | |||
time curve for the break element is given in Figure 6.2.1-92 (Refer to Section 3.8.3.4.9 for pressurizer compartment structural design description). | |||
Reactor Cavity The TMD computer code with the unaugmented homogeneous critical flow correlation and the isentropic compressible subsonic flow correlation was used to calculate pressure transients in the reactor cavity region. | |||
Nodalization sensitivity studies were performed before the analysis was begun. The total number of nodes used varied from 6 to 68. In the 6-element model, no detail of the reactor vessel annulus was involved, and for that reason the model was discarded. | |||
Subsequent model changes primarily involved greater detail in the reactor vessel annulus. First, the annulus was divided into two vertical and eight circumferential regions. Next, some additional detail was added to the region of the broken nozzle. | Subsequent model changes primarily involved greater detail in the reactor vessel annulus. First, the annulus was divided into two vertical and eight circumferential regions. Next, some additional detail was added to the region of the broken nozzle. | ||
The next changes were effected by increasing the model to three vertical and eight circumferential regions. The total integrated pressure in the reactor cavity changed only slightly because of the last change. The next change, to 68 elements, produced the model shown with detailed modeling around the nozzle sustaining the break. The additional elements from 48 to 52 are external to the reactor cavity (ice condenser). Additional elements were added to account for all real area changes in the immediate vicinity of the break (i.e., Elements 53 and 54 were added to model the broken loop pipe annulus and the broken loop inspection port, respectively).The nodal scheme around the reactor vessel produces a very accurate post accident pressure profile because of its design. Element 3 is a small element inside the primary | The next changes were effected by increasing the model to three vertical and eight circumferential regions. The total integrated pressure in the reactor cavity changed only slightly because of the last change. The next change, to 68 elements, produced the model shown with detailed modeling around the nozzle sustaining the break. The additional elements from 48 to 52 are external to the reactor cavity (ice condenser). | ||
Compartments 15, 42, and 16 are really adjoining Compartments 17, 43, and 18, respectively, and Compartment 13 is on the opposite side of the vessel from the assumed break. Element 54 represents the inspection port volume above the break.A break limiting restraint restricts the break size. A 127 | Additional elements were added to account for all real area changes in the immediate vicinity of the break (i.e., Elements 53 and 54 were added to model the broken loop pipe annulus and the broken loop inspection port, respectively). | ||
Richardson.Figures 6.2.1-30 through 6.2.1-68 show representative pressure transients for the break compartments, the upper and lower reactor cavities, the inspection port volume and pipe annulus near the break, the upper containment and the reactor vessel annulus. These plots demonstrate that the pressure gradient is steep near the break location and is very gradual farther away from the break. This indicates that the model must be very detailed close to the break location, but less detail is required with increasing distance (Refer to Section 3.8.3.5.3 for reactor cavity structural design description). | The nodal scheme around the reactor vessel produces a very accurate post accident pressure profile because of its design. Element 3 is a small element inside the primary 6.2.1-32 Containment Functional Design | ||
6.2.1- | |||
(1)The following break types were evaluated.(a)Double-ended 4.6 | WATTS BAR WBNP-112 shield. It would contain internal flow losses due to turning and thus contain a pressure gradient if it were made larger. The four elements numbered 33, 34, 45, and 46 are made small to minimize internal pressure variation, and the elements farther from the break are made larger because pressure gradients are low in those regions. | ||
(3)Failure of a diesel generator is assumed in the containment model for all cases. This results in the loss of one containment safeguards train resulting in minimum heat removal capability. There is no diesel failure associated with the steam line break model. | Figure 6.2.1-27 illustrates the positions of some of the compartments. Figure 6.2.1-28 shows the flow path connections for the 68 element model. Figure 6.2.1-29 illustrates the general configuration of the reactor vessel annulus nodalization. In the model, the lower containment is divided into four loop compartments (21 to 24). The upper containment is represented by Compartment 32. The ice condenser is modeled as five elements (48 to 52), neglecting any flow distribution effects. The break simultaneously occurs in Elements 1 and 25, immediately surrounding the nozzle. The corresponding broken loop pipe annulus is represented by Element 53. The lower reactor cavity is modeled by Element 2, the upper reactor cavity by Element 47, and the remainder of the elements, as shown in Figure 6.2.1-29, model the reactor vessel annulus. | ||
(4)Blowdown from the broken steam line is assumed to be dry saturated steam. | Compartments 15, 42, and 16 are really adjoining Compartments 17, 43, and 18, respectively, and Compartment 13 is on the opposite side of the vessel from the assumed break. Element 54 represents the inspection port volume above the break. | ||
(5)Plant power levels of 100.6% and zero of nominal full-load power for DER, and split pipe ruptures at 30% of nominal full-load power. | A break limiting restraint restricts the break size. A 127 in2 cold leg break is the limiting case break for the reactor cavity analysis. The mass and energy release rates are presented in Table 6.2.1-30. Tables 6.2.1-31 and 6.2.1-32 provide the volumes, flow paths, lengths, diameters, flow areas, resistance factors, and area ratios for the elements and their connections. | ||
(6)Failure of a main steamline isolation valve (MSIV), failure of a feedwater isolation valve (FIV) or control valve (FCV), failure of auxiliary feedwater runout control protection, and failure of a safety injection train are considered. | The inspection port plugs were assumed to be removed at the start of the accident. All insulation is assumed in place and uncrushed during the entire transient except for the insulation between the break and the reactor vessel annulus. This insulation was conservatively assumed to crush to zero thickness. | ||
(7)The auxiliary feedwater system is manually realigned by the operator after 10 minutes to terminate AFW to the faulted steam generator. | The loss coefficient (k) values were determined by changes in flow area and by turns the flow makes in traveling from the centroid of the upstream node to the centroid of the downstream node. The k and f factors for each path were determined using methods from such references as "Flow of Fluids through Valves, Fittings, and Pipes" by the crane company and "Chemical Engineering" by J. M. Coulson and J. A. | ||
Richardson. | |||
(2)Steam Plant Piping | Figures 6.2.1-30 through 6.2.1-68 show representative pressure transients for the break compartments, the upper and lower reactor cavities, the inspection port volume and pipe annulus near the break, the upper containment and the reactor vessel annulus. These plots demonstrate that the pressure gradient is steep near the break location and is very gradual farther away from the break. This indicates that the model must be very detailed close to the break location, but less detail is required with increasing distance (Refer to Section 3.8.3.5.3 for reactor cavity structural design description). | ||
Following the piping blowdown, reverse flow from the intact steam generators continues to simulate the reverse steam generator flow until steam line isolation.Single Failure Effects (1)Failure of the main steam isolation valve (located outside of containment) in the steam line with the break allows steam from all four main steam lines (downstream of the other main steam isolation valves which close) to flow out the break. The analysis accounts for this effect by including an allowance for additional mass and energy released through the break due to the volume of steam contained in the main steam lines. No additional steam is released through the break if the postulated single failure is a main steam isolation valve in another steam line not closing. In this case, the main steam isolation valve in the broken steam line does close and there is no backflow from the downstream piping to the break. | Containment Functional Design 6.2.1-33 | ||
(2)Failure of a feedwater isolation valve could only result in additional inventory in the feedwater line which would not be isolated from the steam generator. | |||
The mass in this volume can flash into the steam generator and exit through the break. The feedwater regulating valve closes in no more than 6.5 seconds precluding any additional feedwater from being pumped into the 6.2.1- | WATTS BAR WBNP-112 6.2.1.3.10 Steam Line Break Inside Containment Pipe Break Blowdowns - Spectra and Assumptions A series of steam line breaks was analyzed to determine the most severe break condition for containment temperature and pressure response. The following assumptions were used in these analyses. | ||
(3)Failure of a feedwater control valve to operate properly can result in an increased feedwater flow into the steam generator and exit through the break. | (1) The following break types were evaluated. | ||
(a) Double-ended 4.6 ft2 ruptures occurring at the nozzle on one steam generator. Steam line flow restrictors in the steam generators limit the effective break area of a full double-ended pipe rupture to a maximum of 1.4 ft2 per steam generator. | |||
(b) The largest split break which will not generate the low steamline pressure signal for steamline isolation. | |||
(c) Small split breaks of 0.6, 0.35, and 0.1 ft2. | |||
(2) Steam line isolation signals and feedwater line isolation signals are generated by either a low steam line pressure signal, high or high-high containment pressure signal, or high steam line pressure rate signal. An allowance of 8 seconds is assumed for steam line isolation including generation, processing, and delay of the isolation signal and valve closure. | |||
An allowance of 8 seconds is assumed for feedwater line isolation including generation, processing, and delay of the isolation signal and valve closure. | |||
(3) Failure of a diesel generator is assumed in the containment model for all cases. This results in the loss of one containment safeguards train resulting in minimum heat removal capability. There is no diesel failure associated with the steam line break model. | |||
(4) Blowdown from the broken steam line is assumed to be dry saturated steam. | |||
(5) Plant power levels of 100.6% and zero of nominal full-load power for DER, and split pipe ruptures at 30% of nominal full-load power. | |||
(6) Failure of a main steamline isolation valve (MSIV), failure of a feedwater isolation valve (FIV) or control valve (FCV), failure of auxiliary feedwater runout control protection, and failure of a safety injection train are considered. | |||
(7) The auxiliary feedwater system is manually realigned by the operator after 10 minutes to terminate AFW to the faulted steam generator. | |||
6.2.1-34 Containment Functional Design | |||
WATTS BAR WBNP-112 (8) For the full double-ended ruptures, the main feedwater flow to the steam generator with the broken steam line was calculated based on an initial flow of 100% of nominal full power flow and a conservatively rapid steam generator depressurization. The peak value of this flow occurring just prior to isolation is 328% of nominal. | |||
Break Flow Calculations (1) Steam Generator Blowdown Break flows and enthalpies from the steam generators are calculated using the Westinghouse LOFTRAN code[14]. Blowdown mass and energy release are determined using the LOFTRAN code which includes effects of core power generation, main and auxiliary feedwater additions, engineered safeguards systems, reactor coolant system thick metal heat storage, and reverse steam generator heat transfer. | |||
(2) Steam Plant Piping Blowdown The contribution to the mass and energy releases from the secondary plant steam piping is included with the mass and energy release rates presented in Table 6.2.1-39. For all ruptures, the steam piping volume blowdown begins at the time of the break and continues at a uniform rate until the entire piping inventory is released. The flowrate is determined using the Moody correlation, the pipe cross-sectional area, and the initial steam pressure. | |||
Following the piping blowdown, reverse flow from the intact steam generators continues to simulate the reverse steam generator flow until steam line isolation. | |||
Single Failure Effects (1) Failure of the main steam isolation valve (located outside of containment) in the steam line with the break allows steam from all four main steam lines (downstream of the other main steam isolation valves which close) to flow out the break. The analysis accounts for this effect by including an allowance for additional mass and energy released through the break due to the volume of steam contained in the main steam lines. No additional steam is released through the break if the postulated single failure is a main steam isolation valve in another steam line not closing. In this case, the main steam isolation valve in the broken steam line does close and there is no backflow from the downstream piping to the break. | |||
(2) Failure of a feedwater isolation valve could only result in additional inventory in the feedwater line which would not be isolated from the steam generator. | |||
The mass in this volume can flash into the steam generator and exit through the break. The feedwater regulating valve closes in no more than 6.5 seconds precluding any additional feedwater from being pumped into the Containment Functional Design 6.2.1-35 | |||
WATTS BAR WBNP-112 steam generator. The additional line volume available to flash into the steam generator is that between the feedwater isolation valve and the feedwater regulating valve. | |||
(3) Failure of a feedwater control valve to operate properly can result in an increased feedwater flow into the steam generator and exit through the break. | |||
Feedwater isolation valve closure limits the feedwater addition to the steam generator. | Feedwater isolation valve closure limits the feedwater addition to the steam generator. | ||
(4)Failure of the auxiliary feedwater runout control equipment would result in higher auxiliary feedwater flows entering the steam generator prior to realignment of the auxiliary feedwater system. For cases where the runout control operates properly, a constant auxiliary feed flow of approximately 1,500 gpm was assumed. This value was increased to approximately 2,250 gpm for the 100% and 0% power cases and 2040 gpm for the 30% power cases to simulate a failure of the runout control. | (4) Failure of the auxiliary feedwater runout control equipment would result in higher auxiliary feedwater flows entering the steam generator prior to realignment of the auxiliary feedwater system. For cases where the runout control operates properly, a constant auxiliary feed flow of approximately 1,500 gpm was assumed. This value was increased to approximately 2,250 gpm for the 100% and 0% power cases and 2040 gpm for the 30% power cases to simulate a failure of the runout control. | ||
(5)Failure of a safety injection train results in less SI flow and will result in a greater return to power. For consistency, with the steam line break core response analysis, the steam line break mass and energy model conservatively assumes failure of a safety injection train.Worst-Case Mass and Energy | (5) Failure of a safety injection train results in less SI flow and will result in a greater return to power. For consistency, with the steam line break core response analysis, the steam line break mass and energy model conservatively assumes failure of a safety injection train. | ||
(1)Full double-ended rupture at 100.6% of nominal full power with a failure of the AFW runout control system. This represents the limiting DER case in terms of calculated peak temperature. | Worst-Case Mass and Energy Releases The following steam line break cases were determined to represent the worst case steamline break results. | ||
(2)A 0.6 | (1) Full double-ended rupture at 100.6% of nominal full power with a failure of the AFW runout control system. This represents the limiting DER case in terms of calculated peak temperature. | ||
(3)A 0.35 | (2) A 0.6 ft2 split break at 30% of nominal full power with a failure of the AFW runout control system. This represents the limiting SB case in terms of calculated peak temperature. | ||
[3] with the following restrictions. | (3) A 0.35 ft2 split break at 30% at nominal full power with a failure of the AFW runout control system. This represents the limiting SB case in terms of superheat temperature duration. | ||
(1)Mass and energy release rates are calculated with an approved model. | Mass and energy releases for these cases are listed in Table 6.2.1-39. | ||
(2)Complete break spectrums are analyzed. | Maximum Containment Temperature Analysis for Steam Line Break Following a steam line break in the lower compartment of an ice condenser plant, two distinct analyses must be performed. The first analysis, a short-term pressure analysis, has been performed with the TMD computer code (see Section 6.2.1.3.9). | ||
(3)Convective heat flux calculations, as described in References [2] and [27], are performed for all break sizes.For the worst case steam line breaks, one condensation model is | The second analysis, a long-term analysis, does not require the large number of nodes 6.2.1-36 Containment Functional Design | ||
(1)Minimum safeguards are employed, e.g., one of two spray pumps, and one of two air return fans. | |||
(2)A quantity of 2. | WATTS BAR WBNP-112 which the TMD analysis requires. The computer code which performs this analysis is the LOTIC computer code. | ||
(3)The boron injection tank remains installed without heat tracing, and the boric acid concentration is reduced to zero ppm (Table 6.2.1-40). | The LOTIC-3 computer code was developed to analyze steamline breaks in an ice condenser plant. Details of the LOTIC-3 computer code are given in Reference [3]. It includes the capability to calculate superheat conditions, and has the ability to begin calculations from time zero. The LOTIC-3 computer code has been found to be acceptable for the analysis of steam line breaks[3] with the following restrictions. | ||
(4)The air return fan is effective 10 minutes after the transient is | (1) Mass and energy release rates are calculated with an approved model. | ||
(5)A uniform distribution of steam flow into the ice bed is assumed. | (2) Complete break spectrums are analyzed. | ||
(6)The initial conditions in the containment are a temperature of 120°F in the lower compartment, 120°F in the dead-ended compartment, a temperature of 85°F in the upper compartment, and a temperature of 32°F in the ice condenser. All volumes (see Table 6.2.1-13) are at a pressure of 0.3 psig . | (3) Convective heat flux calculations, as described in References [2] and [27], | ||
(7)A containment spray pump flow of 4,000 gpm is conservatively used in the upper compartment. A diesel loading sequence for the containment sprays to energize and come up to full flow and head in 234 seconds was used in the analysis. | are performed for all break sizes. | ||
6.2.1- | For the worst case steam line breaks, one condensation model is used by the LOTIC-3 computer code. For these three breaks, the conservative 0% condensate reevaporization and convective heat flux model is used. | ||
(9)The air return fan empties air at a rate of 40,000 | Containment Transient Calculations The following are the major input assumptions used in the LOTIC-3 steamline break analysis for the Watts Bar Nuclear Plant. | ||
(10)A series of large break cases (1.4 | (1) Minimum safeguards are employed, e.g., one of two spray pumps, and one of two air return fans. | ||
(11)The mass and energy releases for the limiting breaks are given in Table 6.2.1-39. Since these rates are considerably less than the RCS double-ended breaks and their total integrated energy is not sufficient to cause icebed meltout, the containment pressure transients generated for the RCS breaks will be more severe. However, since the steam line break blowdowns are superheated, the lower compartment temperature transients calculated in this analysis will be limited. These temperature transients are given in Figures 6.2.1-69 through 6.2.1-74. | (2) A quantity of 2.125x106 lbs of ice is assumed for the steamline break cases to be initially in the ice condenser. | ||
(12)The heat transfer coefficients to the containment structures are based on the work of Tagami. An explanation of their manner of application is given in Reference [3]. The stagnant heat transfer coefficients were limited to 72 Btu/hr- | (3) The boron injection tank remains installed without heat tracing, and the boric acid concentration is reduced to zero ppm (Table 6.2.1-40). | ||
(4) The air return fan is effective 10 minutes after the transient is initiated. Actual air return fan initiation can take place in 9+1 minutes. Initiation as early as 8 minutes does not adversely affect the outcome of the analysis. | |||
6.2.1.3.11 | (5) A uniform distribution of steam flow into the ice bed is assumed. | ||
(1)The initial blowdown, which occurs in approximately 10 seconds. During this period, the air initially in the lower compartment is swept into the upper compartment and the dead-ended compartment by the blowdown mass. | (6) The initial conditions in the containment are a temperature of 120°F in the lower compartment, 120°F in the dead-ended compartment, a temperature of 85°F in the upper compartment, and a temperature of 32°F in the ice condenser. All volumes (see Table 6.2.1-13) are at a pressure of 0.3 psig . | ||
(7) A containment spray pump flow of 4,000 gpm is conservatively used in the upper compartment. A diesel loading sequence for the containment sprays to energize and come up to full flow and head in 234 seconds was used in the analysis. | |||
Containment Functional Design 6.2.1-37 | |||
WATTS BAR WBNP-112 (8) Containment structural heat sinks as presented in Table 6.2.1-1 were used. | |||
The material properties are given in Table 6.2.1-5. | |||
(9) The air return fan empties air at a rate of 40,000 ft3/min from the upper to the lower compartments. The total calculated air flow rate discharged to the dead-end compartment used is 41,885 cfm and is, therefore, bounded. | |||
(10) A series of large break cases (1.4 ft2 double-ended ruptures) was run to determine the limiting large break case (Table 6.2.1-41). In addition, a series of small breaks was analyzed with LOTIC at the 30% power level (Table 6.2.1-42). | |||
(11) The mass and energy releases for the limiting breaks are given in Table 6.2.1-39. Since these rates are considerably less than the RCS double-ended breaks and their total integrated energy is not sufficient to cause icebed meltout, the containment pressure transients generated for the RCS breaks will be more severe. However, since the steam line break blowdowns are superheated, the lower compartment temperature transients calculated in this analysis will be limited. These temperature transients are given in Figures 6.2.1-69 through 6.2.1-74. | |||
(12) The heat transfer coefficients to the containment structures are based on the work of Tagami. An explanation of their manner of application is given in Reference [3]. The stagnant heat transfer coefficients were limited to 72 Btu/hr-ft2. This corresponds to a steam-air ratio of 1.4 (according to the Tagami correlation). The imposition of this limitation is to restrict the use of the Tagami correlation within the range of steam-air ratios from which the correlation was derived. | |||
The containment responses presented identify the limiting and most severe cases for the large double-ended ruptures and small split breaks. | |||
Large Break The limiting case among the double-ended ruptures, which yielded a calculated peak temperature of 323.9°F and a peak pressure of 9.29 psig, is the 1.4 ft2 loop break at 100.6% of nominal full power with a failure of the AFW runout control system. Figure 6.2.1-69 provides the upper and lower compartment temperature transients, and Figure 6.2.1-70 illustrates the lower compartment pressure transients. Table 6.2.1-39 contains the mass and energy release rates for the above case. | |||
Small Break The most severe transient in terms of superheat temperature duration for the small break spectrum is the 0.35 ft2, 30% nominal full power, with AFW pump runout protection failure. The temperature transient with a peak temperature of 324.4°F and peak pressure of 6.58 psig for the case is presented in Figure 6.2.1-71, and the pressure transient is provided in Figure 6.2.1-72. Table 6.2.1-39 provides the mass and energy release rates for this case. | |||
6.2.1-38 Containment Functional Design | |||
WATTS BAR WBNP-112 The most limiting case in terms of peak calculated temperature is the 0.6 ft2, 30% | |||
power, with AFW pump runout protection failure. This case resulted in a calculated peak temperature of 325.1°F and peak pressure of 6.83 psig. Figure 6.2.1-73 presents the temperature transient, and Figure 6.2.1-74 shows the pressure transient of the lower compartment. The mass and energy releases are provided in Table 6.2.1-39. | |||
Tables 6.2.1-43 and 6.2.1-44 provide the overall results of the calculated peak temperatures for the large and small break spectrums, respectively. | |||
6.2.1.3.11 Maximum Reverse Pressure Differentials Following a postulated pipe break accident, the occurrence inside the ice condenser containment may be characterized by two distinct periods: | |||
(1) The initial blowdown, which occurs in approximately 10 seconds. During this period, the air initially in the lower compartment is swept into the upper compartment and the dead-ended compartment by the blowdown mass. | |||
Large mass and pressure gradients occur throughout the containment. | Large mass and pressure gradients occur throughout the containment. | ||
(2)The depressurization and post-blowdown period which occurs after the end of the initial blowdown. During this period the pressure gradient within the four compartments (upper, lower, ice condenser, and dead-ended) is almost nonexistent. The shape of the pressure transient resembles that of the mass and energy releases. Pressure decreases as blowdown diminishes, followed by a slow increase sometime during the reflood.The analysis for the first period will usually require the modeling of the containment into many nodes so that the non-uniformity of pressure and mass distribution may be properly represented. This has been done in the TMD code.On the other hand, the analysis for the second period will only require the modeling of the containment by a four-compartment system. These calculations are performed by the LOTIC code [1, 28].The code options and features discussed are used in calculating ECCS back-pressure and reverse pressure differentials across the operating deck.Basic Assumptions (1)The containment is assumed to be physically divided into four compartments: | (2) The depressurization and post-blowdown period which occurs after the end of the initial blowdown. During this period the pressure gradient within the four compartments (upper, lower, ice condenser, and dead-ended) is almost nonexistent. The shape of the pressure transient resembles that of the mass and energy releases. Pressure decreases as blowdown diminishes, followed by a slow increase sometime during the reflood. | ||
(2)Flow between compartments is related to the pressure differential between the compartments by a flow resistance factor. | The analysis for the first period will usually require the modeling of the containment into many nodes so that the non-uniformity of pressure and mass distribution may be properly represented. This has been done in the TMD code. | ||
(3)A two-sump model is assumed. Temperature is considered to be uniform in each sump. | On the other hand, the analysis for the second period will only require the modeling of the containment by a four-compartment system. These calculations are performed by the LOTIC code [1, 28]. | ||
6.2.1- | The code options and features discussed are used in calculating ECCS back-pressure and reverse pressure differentials across the operating deck. | ||
(1)Energy equation:For the lower compartment: | Basic Assumptions (1) The containment is assumed to be physically divided into four compartments: | ||
upper, lower, ice condenser, and dead-ended compartments. Each compartment is a control volume of uniform temperature, pressure and mass distribution. Steam is also assumed to be saturated in each control volume. | |||
- [Rate of flow energy of sprays if applicable] | (2) Flow between compartments is related to the pressure differential between the compartments by a flow resistance factor. | ||
- [Rate of heat transfer to the sump] | (3) A two-sump model is assumed. Temperature is considered to be uniform in each sump. | ||
- [Rate of heat removal by the ice condenser drain flow, if acting as a spray]- [Rate of energy associated with the loss on condensate from atmosphere falling to floor]+ [Net rate of flow energy from the dead-ended compartment]For the upper compartment: | Containment Functional Design 6.2.1-39 | ||
WATTS BAR WBNP-112 Conservation Equations For each control volume or compartment, the conservation equations of mass, energy, momentum, and volume, an ideal gas law for air, and the equation of state for saturated steam may be written: | |||
(1) Energy equation: | |||
d- ( V as + V c ) d ( P s + P a ) | |||
---- (M a h a + M s h s + M c h c) - --------------------------- ------------------------------ + ( mh ) out - ( mh ) in = R e dt J dt For the lower compartment: | |||
Re = [Rate of energy out of break] | |||
+ [Rate of flow energy from accumulator in the form of steam, water, and nitrogen] | |||
- [Rate of structural heat removal] | |||
- [Rate of flow energy of sprays if applicable] | |||
- [Rate of heat transfer to the sump] | |||
- [Rate of heat removal by the ice condenser drain flow, if acting as a spray] | |||
- [Rate of energy associated with the loss on condensate from atmosphere falling to floor] | |||
+ [Net rate of flow energy from the dead-ended compartment] | |||
For the upper compartment: | |||
Re = [Flow energy of the entering spray] | |||
- [Structure heat removal rate] | |||
- [Energy rate associated with condensate falling from atmosphere] | |||
For the ice condenser: | |||
Re =[Structure heat removal rate] | |||
- [Rate of heat transfer to the ice] | |||
- [Energy rate associated with ice melt and steam condensate falling from atmosphere] | |||
(2) Conservation of steam and water masses: | |||
dM s dM c | |||
----------- + ----------- + ( M s ) - ( M s ) in = R s dt dt out 6.2.1-40 Containment Functional Design | |||
WATTS BAR WBNP-112 For the lower compartment: | |||
Rs = [Rate of flow out of the RCS] | |||
+ [Rate of flow out of the accumulator in the form of steam and water] | |||
+ [Flow rate of the entering spray if applicable] | |||
- [Rate of condensate falling to the floor] | |||
+ [Rate of steam flow from the dead-ended compartment] | |||
For the upper compartment: | |||
Rs = [Flow rate of the entering spray] | |||
- [Rate of condensate falling to the floor] | |||
For the ice condenser: | |||
Rs = - [Rate of condensate falling to the floor] | |||
(3) Conservation of air mass: | |||
dM | |||
----------a- + ( M a ) - ( M a ) in = R a dt out For the lower compartment: | |||
Ra = [Rate of nitrogen flow out of the accumulator] | |||
+ [Rate of air flow out of the dead-ended compartment] | |||
For the upper compartment and the ice condenser: | |||
Ra = 0 (4) Conservation of momentum: | |||
2 1 K M ij P i - P j = --- -----ij- --------- | |||
2 A 2 g c | |||
(5) Volume conservation: | |||
dV as dV c | |||
------------- + ---------- = R v dt dt Containment Functional Design 6.2.1-41 | |||
WATTS BAR WBNP-112 For the lower compartment: | |||
Rv = [Rate of increase in sump water volume] | |||
For the upper compartment: | |||
Rv = 0 For the ice condenser: | |||
Rv = [Rate of increase in free volume due to ice melting] | |||
(6) Ideal gas law for air: | |||
PaVas = MaRaT (7) Equations of state for saturated steam: | |||
Ps = f1(T), hs = f2(T), vs = f3(T) | |||
For the dead-ended compartment, the structure heat removal is assumed to be negligible, and the conservation equations of energy and mass simplified to: | |||
d v d ( Ps + Pa ) | |||
----- ( M a h a + M s h s ) - --- --------------------------- | |||
- = [ Rate of energy flow from the lower compartment ] | |||
dt J dt | |||
( dM a ) | |||
------------------ = [Rate of air flow from the lower compartment] | |||
dt | |||
( dM s ) | |||
---------------- = [Rate of steam flow from the lower compartment] | |||
dt Method of Solution The preceding equations were linearized and programmed for simultaneous solutions using the standard Gauss-Jordan reduction method. For each time step, the solutions are the rates of increase of mass and pressure for each constituent in each compartment, and the flow rates between the compartments. These rates are used to control the time step so that total change of the compartment conditions in each time step can be controlled. This assures more accurate and stable solutions. | |||
Structure Heat Transfer The standard Westinghouse ECCS containment structural heat transfer model is applied to this code. This model assumes one dimensional conduction heat transfer in the structure and uses film heat transfer coefficient based primarily on the work of Tagami. The Tagami correlation for the film heat transfer may be written as: | |||
6.2.1-42 Containment Functional Design | |||
WATTS BAR WBNP-112 E 0.6 H max = 75 -------- (1) tp V t | |||
H = H max = -------- for 0 t t p (2) tp | |||
- 0.5 [ t - t p ] | |||
H = H stag + [ H max - H stag ]e for t p t (3) where: | |||
-- | H stag = 2 + 50 X (4) | ||
For this application, we have found it is useful to relate the "coolant energy transfer", | |||
(E/tpV), to containment conditions. This may be done by writing: | |||
E Ms hs + Mf hf 1 M | |||
- = ---------- h s + -------f h f | |||
-------- = ------------------------------- (5) tp V tp V tp vs Ms where: | |||
h s, h f and vs are respectively the enthalpies of saturated steam and water, and the specific volume of steam, at tp, the time when the peak containment pressure is reached. | |||
Equations (1) through (5) are used for the lower compartment structure calculations. | |||
For the upper compartment, only the stagnant heat transfer correlation of Equation (4) is used because of little steam penetration into the upper compartment even during the initial blowdown period. | |||
Ice Condenser Heat Transfer The transfer of heat from steam to ice which results in the simultaneous occurrence of steam condensation and ice melting is a complex mechanism. | |||
During the initial blowdown period when high temperature blowdown steam and water hits the bottom of ice columns, and then flows over the ice surface, turbulent condensation results. During this period the heat transfer rate is strongly dependent on the thickness of the liquid film which separates the high temperature blowdown masses from the ice. This liquid film is composed of steam condensate and ice melt. | |||
On the macroscopic scale, this is the only heat transfer resistance and the Containment Functional Design 6.2.1-43 | |||
WATTS BAR WBNP-112 effectiveness of the ice condenser is determined by the rate which this liquid film may be withdrawn. A semi-empirical model for the ice condenser heat transfer during this period is available and has been used successfully in the TMD code. The LOTIC code is not intended to duplicate this effort. Instead mass and energy balances are used to calculate the total ice melting during this period. Following the initial blowdown period, there is a transition period when the blowdown mass and energy rates are decreasing rapidly and the containment atmosphere as a whole is losing internal energy. | |||
Depressurization and decreasing compartment temperature generally characterize this transition period. As the containment conditions lapse into a much more stable and slowly changing pace after the transition period, the blowdown from the broken pipe is almost drawing to an end. Flow in the ice condenser is now at a rate which is almost negligible compared to that in the initial blowdown period. Temperature in the ice condenser atmosphere has also decreased. Thus, heat transfer is governed by combining natural convection and steam diffusion through an almost stagnant atmosphere. Due to the large air content, the resistance to diffusion is large. | |||
( | Therefore, most of the temperature difference between the free-steam steam-air mixture and the ice occurs between the free-steam and the free surface of the liquid film. Temperature difference across the liquid film is now comparatively small. Due to the loss of dominance for the liquid film resistance in the overall heat transfer mechanism, it is not surprising for Yen, Zender, Zavohik, and Tien[11] to conclude that ice melting has very little effect on the overall heat transfer coefficient for condensation-melting heat transfer in the presence of a substantial air concentration. From this, we may therefore treat the ice as if it were simply a cold structure and use Equation (4) to calculate the heat transfer coefficient after the transition period. | ||
During the transition period, it is plausible to assume that the ice condenser is capable of maintaining its internal energy by condensing any excess energy which flow into the ice condenser. | |||
Special Code Capabilities in Response to Previous NRC Concerns (1) Heat removal from the lower compartment by the ice condenser drain may be accounted for by input of a spray-like efficiency. | |||
(2) Heat transfer between the lower compartment atmosphere and the sump surface can also be taken into account. | |||
Drains are provided at the bottom of the ice condenser compartment to allow the melt/condensate water to flow out of the compartment during a loss of coolant accident. In the modified LOTIC code, a calculation of the flow rate at which water leaves these ice condenser drains is included. The solution was reached by using the hydraulic incompressible flow equations commonly found in the literature for both filled pipe flow and fall (weir) flow conditions and at any point in time using the minimum flow rate calculated by the two methods. The filled pipe flow equation employed was a simplified Bernoulli balance: | |||
6.2.1-44 Containment Functional Design | |||
WATTS BAR WBNP-112 2 | |||
V Z 1 = ----- + h f + Z 2 2g where: | |||
Z = Elevation V = Velocity g = Gravitational constant | |||
= Density V 22 fl- ------ | |||
- | hf = ----- | ||
6.2.1- | * g sd 2 Subscripts 1 and 2 represent conditions at the inlet and outlet of the drain, respectively. | ||
The area of the ice condenser sump was taken to be 3170 ft2, and the height of the door sill to be 8.75 inches. After calculating the velocity from the previous equation, the mass flow rate can be calculated from | |||
* = V A m 2 2 Since a filled pipe flow condition may not exist during the entire post accident transient, a calculation of the draining rate based on the existence of a fall flow phenomena was included. The corresponding equations are outlined below, 2 | |||
Q = --- 2g ( H e3 2 - h 13 2 ) | |||
3 where: | |||
Q = Discharge per foot of width (ft3/sec-ft) | |||
He = Energy of fluid upstream of the fall h1 = Energy of the fluid at the fall edge minus the flowing height D1 = 0.643 Dc h1 = He - D1 By assuming the approach velocity equals zero and through substitution, we arrive at the simplified equation: | |||
Containment Functional Design 6.2.1-45 | |||
WATTS BAR WBNP-112 2 | |||
Q = --- 2g [ D c3 2 - ( 0.357 D c) 3 2] | |||
3 or Q = 4.2088 D c3 2 where: | |||
Dc = ft. | |||
Calculation of Maximum Reverse Pressure Differential The computer model previously described was used to calculate the reverse differential pressure across the operating deck. In order to calculate a maximum reverse differential pressure the following assumptions were made: | |||
(1) The dead-ended compartment volumes adjacent to the lower compartment (fan and accumulator rooms, pipe trenches, etc.) were assumed to be swept of air during the initial blowdown. This is a very conservative assumption, since this will maximize the air mass forced into the upper ice bed and upper compartment thus raising the compression pressure. In addition, it will minimize the mass of the noncondensables in the lower compartment. With this modeling the dead-ended volume is included with that of the lower compartment (see Figure 6.2.1-75), resulting in a 3-volume simulation of the containment. | |||
(2) The minimum containment temperatures are assumed in the various subcompartments. This will maximize the air mass forced into the upper containment. It will also increase the heat removal capability of the cold lower compartment structures. | |||
(3) An RWST temperature of 100°F is assumed. This will help raise the upper containment temperature and pressure higher for a longer period of time. The current maximum RWST temperature is 105°F, which has a negligible effect. | |||
(See Table 6.2.1-37.) | |||
(4) The upper containment spray flowrates used were runout flows. | |||
(5) Containment spray to the upper compartment was assumed to start at 25 seconds. An early start time is conservative in that it raises the upper compartment temperature and pressure when the air mass in the upper compartment is at its highest value. Containment spray initiation to the upper containment is tabulated in Table 6.2.1-25. An increased delay should have no negative effect on the maximum reverse pressure differential. | |||
(6) The containment geometry is the same as that used in the minimum pressure analysis for ECCS purposes. (See Tables 6.2.1-33 through 6.2.1-36.) | |||
6.2.1-46 Containment Functional Design | |||
WATTS BAR WBNP-112 (7) The Westinghouse ECCS model (see WCAP-8339) was used for heat transfer to the structure. | |||
(8) The mass and energy releases used are based on the analysis presented in WCAP-8479. | |||
(9) Ice condenser doors are assumed to act as check valves, allowing flow only into the ice condenser. | |||
(10) The loss coefficient (k/A2) of the deck fins for air flow from the upper to the lower compartment was taken to be 0.0072 ft-4. This value was based on the capabilities of the fans while running. With the fans not running the loss coefficient would be 0.0278 ft-4. | |||
With these assumptions the maximum reverse pressure differential across the operating deck was calculated to be 0.65 psi. The following plots have been provided: | |||
Figure 6.2.1-76 which shows upper and lower compartment pressures. | |||
(8)The mass and energy releases used are based on the analysis presented in WCAP-8479. | |||
(9)Ice condenser doors are assumed to act as check valves, allowing flow only into the ice condenser. | |||
(10)The loss coefficient (k/ | |||
-4. This value was based on the capabilities of the fans while running. With the fans not running the loss coefficient would be 0.0278 ft | |||
-4.With these assumptions the maximum reverse pressure differential across the operating deck was calculated to be 0.65 psi. The following plots have been provided:Figure 6.2.1-76 which shows upper and lower compartment pressures. | |||
Figure 6.2.1-77 which shows upper and lower compartment temperatures. | Figure 6.2.1-77 which shows upper and lower compartment temperatures. | ||
Figure 6.2.1-78 which shows upper to lower compartment flowrates.Parametric studies have been made with this model. Various effects have been investigated to determine changes in the maximum reverse pressure differential. Table 6.2.1-37 gives some of these studies with their results. For Case 6, Figures 6.2.1-79 and 6.2.1-80 give plots similar to Figures 6.2.1-76 and 6.2.1-77. Presented in Table 6.2.1-38, also for Case 6, are the sump temperature and the steam exit flow from the ice condenser, both as a function of time.Significant margin exists between the design reverse differential pressures across the operating deck and the ice condenser lower inlet doors and those calculated pressures presented in Table 6.2.1-37. | Figure 6.2.1-78 which shows upper to lower compartment flowrates. | ||
Parametric studies have been made with this model. Various effects have been investigated to determine changes in the maximum reverse pressure differential. | |||
(2)"Final Report Ice Condenser Full-Scale Section Tests at the Waltz Mill Facility", WCAP-8282, February 1974 (Proprietary). | Table 6.2.1-37 gives some of these studies with their results. For Case 6, Figures 6.2.1-79 and 6.2.1-80 give plots similar to Figures 6.2.1-76 and 6.2.1-77. Presented in Table 6.2.1-38, also for Case 6, are the sump temperature and the steam exit flow from the ice condenser, both as a function of time. | ||
(3) | Significant margin exists between the design reverse differential pressures across the operating deck and the ice condenser lower inlet doors and those calculated pressures presented in Table 6.2.1-37. | ||
(4)"Ice Condenser Containment Pressure Transient Analysis Method," WCAP-8078, March 1973 (Non-Proprietary). | Nomenclature SYMBOL DESCRIPTION A Flow area E Total energy J Conversion constant, 778 ft-lbf/Btu K Flow resistance factor M Mass P Pressure R Gas constant R Rate Containment Functional Design 6.2.1-47 | ||
(6)Deleted by Amendment 85. | |||
(7)Deleted by Amendment 85. | WATTS BAR WBNP-112 SYMBOL DESCRIPTION T Temperature V Volume gc Conversion constant, 32.2 ft-lbm/lbf-sec2 h Enthalpy m Mass flow rate between two compartments t Time x Steam-air ratio v Specific volume Density SUBSCRIPT a Air as Air and steam c Suspended or entrained water e Energy i i-th compartment j j-th compartment ij from i-th compartment to j-th compartment s Steam REFERENCES (1) Long Term Ice Condenser Containment Code - LOTIC Code, WCAP-8354-P-A, April 1976 (Proprietary), WCAP-8355A, April 1976 (Non-proprietary). | ||
(8)Deleted by Amendment 85. | (2) "Final Report Ice Condenser Full-Scale Section Tests at the Waltz Mill Facility", WCAP-8282, February 1974 (Proprietary). | ||
(9) | (3) Westinghouse Long-Term Ice Condenser Containment Code - LOTIC-3 Code, WCAP-8354-P-A S2, February 1979 (Proprietary), WCAP-8355-NP-S2, February 1979 (Non-Proprietary). | ||
(4) "Ice Condenser Containment Pressure Transient Analysis Method," | |||
WCAP-8078, March 1973 (Non-Proprietary). | |||
6.2.1-48 Containment Functional Design | |||
WATTS BAR WBNP-112 (5) Test Plans and Results for the Ice Condenser System, Ice Condenser Full-Scale Section Test at the Waltz Mill Facility, WCAP-8110-S6, May 1974 (Non-proprietary). | |||
(6) Deleted by Amendment 85. | |||
(7) Deleted by Amendment 85. | |||
(8) Deleted by Amendment 85. | |||
(9) Topical Report Westinghouse Mass and Energy Release Data for Containment Design, WCAP-8264-P-A, Rev. 1, August 1975 (Proprietary), | |||
WCAP-8312-A, Rev. 2 (Non-proprietary). | WCAP-8312-A, Rev. 2 (Non-proprietary). | ||
(10)Deleted by Amendment 85. | (10) Deleted by Amendment 85. | ||
(11)Yen, Y. C., Zender, A., Zavohik, S. and Tien, C., "Condensation - Melting Heat Transfer in the Presence of Air," Thirteenth National Heat Transfer Conference, AICHE - ASME Denver. | (11) Yen, Y. C., Zender, A., Zavohik, S. and Tien, C., "Condensation - Melting Heat Transfer in the Presence of Air," Thirteenth National Heat Transfer Conference, AICHE - ASME Denver. | ||
(12)Crane Technical Paper #410, "Flow of Fluid." (13)"Electrical Hydrogen Recombiner for PWR Containments," WCAP-7709-P-A (Proprietary) and WCAP-7820-A (Non-Proprietary) and Supplements 1, 2, 3, and 4.(14)Burnett, T. W. T., et al, "LOFTRAN Code Description," WCAP-7907-P-A (Proprietary), April 1984, WCAP-7907-A (Non-Proprietary), April 1984. | (12) Crane Technical Paper #410, "Flow of Fluid." | ||
(15)King, H. W., "Handbook of Hydraulics," 4th Edition, 1954. | (13) "Electrical Hydrogen Recombiner for PWR Containments," WCAP-7709-P-A (Proprietary) and WCAP-7820-A (Non-Proprietary) and Supplements 1, 2, 3, and 4. | ||
(16)Deleted by Amendment 97. | (14) Burnett, T. W. T., et al, "LOFTRAN Code Description," WCAP-7907-P-A (Proprietary), April 1984, WCAP-7907-A (Non-Proprietary), April 1984. | ||
(17)Deleted by Amendment 97. | (15) King, H. W., "Handbook of Hydraulics," 4th Edition, 1954. | ||
(18)Deleted by Amendment 97. | (16) Deleted by Amendment 97. | ||
(19)US NRC Regulatory Guide 1.7, Rev. 2, November 1978, "Control of Combustible Gas Concentrations in Containment Following a Loss of Coolant Accident." (20)"Westinghouse LOCA Mass and Energy Release Model for Containment Design March 1979 Version," WCAP-10325-P-A, May 1983 (Proprietary), WCAP-10326-A May 1983 (Non-proprietary). | (17) Deleted by Amendment 97. | ||
(21) | (18) Deleted by Amendment 97. | ||
6.2.1- | (19) US NRC Regulatory Guide 1.7, Rev. 2, November 1978, "Control of Combustible Gas Concentrations in Containment Following a Loss of Coolant Accident." | ||
(23)Docket No. 50-315, "Amendment No. 126, Facility Operating License No. DPR-58 (TAC No. 71062), D. C. Cook Nuclear Plant Unit 1," June 9, 1989. | (20) "Westinghouse LOCA Mass and Energy Release Model for Containment Design March 1979 Version," WCAP-10325-P-A, May 1983 (Proprietary), | ||
(24) | WCAP-10326-A May 1983 (Non-proprietary). | ||
(25)ANSI/ANS-5.1-1979, | (21) Interim Report on Safety Assessments and Facilities Establishment Project in Japan for Period Ending June 1965 (No. 1), Tagami, Takasi. | ||
(26)W. H. McAdams, Heat Transmission, McGraw-Hill | Containment Functional Design 6.2.1-49 | ||
(27) | |||
(28) | WATTS BAR WBNP-112 (22) "Topical Report Westinghouse ECCS Evaluation Model 1981 Version," | ||
WCAP-9220-P-A, Revision 1, February 1982 (Proprietary), WCAP-9221-A, Revision I, February 1982 (Non-Proprietary). | |||
(23) Docket No. 50-315, "Amendment No. 126, Facility Operating License No. | |||
DPR-58 (TAC No. 71062), D. C. Cook Nuclear Plant Unit 1," June 9, 1989. | |||
(24) Mixing of Emergency Core Cooling Water with Steam: 1/3-Scale Test and Summary, WCAP-8423, June 1975 (Proprietary). | |||
(25) ANSI/ANS-5.1-1979, American National Standard for Decay Heat Power in Light Water Reactor, August 29, 1979. | |||
(26) W. H. McAdams, Heat Transmission, McGraw-Hill 3rd edition, 1954, p. 172. | |||
(27) Answers to AEC Questions on Report WCAP-8282, WCAP-8282-AD1, May 1974 (Proprietary). | |||
(28) Long Term Ice Condenser Containment Code - LOTIC Code, WCAP-8354-P-A-S1, April 1976 (Proprietary), WCAP-8355-A-S1, April 1976 (Non-proprietary). | |||
6.2.1-50 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-1 Structural Heat Sinks (Page 1 of 2) | |||
A. Upper Compartment Area Thickness Material (ft2) (ft) | |||
: 1. Operating Deck Slab 1 4880 1.066 Concrete Slab 2 18280 0.0055 Paint 1.4 Concrete Slab 3 760 0.0055 Paint 1.5 Concrete Slab 4 3840 0.0208 Stainless Steel 1.5 Concrete 2.Shell and Misc Slab 5 56331 0.001 Paint 0.079 Steel B. Lower Compartment | |||
: 1. Operating Deck, Crane Wall, and Interior Concrete Slab 6 31963 1.43 Concrete | |||
: 2. Operating Deck Slab 7 2830 0.0055 Paint 1.1 Concrete Slab 8 760 0.0055 Paint 1.75 Concrete | |||
: 3. Interior Concrete and Stainless Steel Slab 9 2270 0.0208 Stainless Steel 2.0 Concrete | |||
: 4. Floor* | |||
Slab 10 15921 0.0055 Paint 1.6 Concrete | |||
: 5. Misc Steel Slab 11 28500 0.001 Paint 0.0656 Steel Containment Functional Design 6.2.1-51 | |||
WATTS BAR WBNP-112 Table 6.2.1-1 Structural Heat Sinks (Page 2 of 2) | |||
Area Thickness Material (ft2) (ft) | |||
C. Ice Condenser | |||
: 1. Ice Baskets Slab 12 149,600 0.00663 Steel | |||
: 2. Lattice Frames Slab 13 75,865 0.0217 Steel | |||
: 3. Lower Support Structure Slab 14 28,670 0.0587 Steel | |||
: 4. Ice Condenser Floor Slab 15 3,336 0.0055 Paint 0.33 Concrete | |||
: 5. Containment Wall Panels & Containment Shell Slab 16 19,100 1.0 Steel & Insulation 0.0625 Steel Shell | |||
: 6. Crane Wall Panels and Crane Wall Slab 17 13,055 1.0 Steel & Insulation 1.0 Concrete | |||
* In contact with sump. | |||
6.2.1-52 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-2 Pump Flow Rates Vs. Time (Time Sequence to Switchover from Injection to Recirculation) | |||
Time after HHSI RHR CSS RHR Safeguards Pump Pump Pump Spray Sump RWST Initiation CCP Flow Flow Flow Flow Flow Flowrate Flowrate (sec) (gpm) (gpm) (gpm) (gpm) (gpm) (gpm) (gpm) | |||
SI Signal 0 0 0 0 0 0 0 0 Initiated CCP Starts and 12 560 0 0 0 0 0 560 Reaches Rated Flow HHSI Pump 17 560 675 0 0 0 0 1235 Starts and Reaches Rated Flow RHR Pump Starts 22 560 675 5500 0 0 0 6735 and Reaches Rated Flow CSS Pump Starts 234 560 675 5500 4950 0 0 11685 and Reaches Rated Flow RWST Low Level 1207.3 560 675 5500 4950 0 0 11685 Alarm, Automatic Realignment of RHR Sump Valves 1267.3 560 675 2750 4950 0 2750 6185 Open, RWST to RHR Valves Close HHSI & CCP 1344.3 560 675 2750 4950 0 2750 4950 Suction Valves from RHR Discharge Open Low-Low RWST 2588.7 560 675 2750 4950 0 2750 4950 Level Alarm Shut Off CSS 2598.7 560 675 2750 0 0 2750 0 Pump Restart CSS 2718.7 560 675 2750 0 0 2750 0 Pump Start RHR Spray 3600 560 675 2750 4950 2000 2750 0 Containment Functional Design 6.2.1-53 | |||
WATTS BAR WBNP-112 Table 6.2.1-3 Energy Balances Approx. End of Blowdown Approx. End of Reflood Sink (t = 10.0 sec) (t=243.4 sec) | |||
(Millions of BTUs) | |||
Ice Heat Removal* 190.811 246.406 Structural Heat Sinks* 17.686 57.676 RHR Heat Exchanger Heat Removal* 0.0 0.0 Spray Heat Exchanger Heat Removal* 0.0 0.0 Energy Content of Sump** 173.409 229.192 Ice Melted (millions of lbm) 0.6160 0.8386 | |||
*Integrated Heat Rates | |||
**Energy Content of Sump Includes Active and Inactive Regions 6.2.1-54 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-4 Energy Balances Ice Meltout Time Approx. Time of Approx. Peak Pressure (t=2659.8 sec) (t=4348.6 sec) | |||
(Millions of BTUs) | |||
Ice Heat Removal* 601.367 601.389 Structural Heat Sinks* 68.084 100.780 RHR Heat Exchanger Heat Removal* 18.566 38.875 Spray Heat Exchanger Heat Removal* 0.0 32.176 Energy Content of Sump** 597.741 595.857 Ice Melted (millions of lbs) 2.2599 2.2600 | |||
*Integrated Heat Rates | |||
**Energy Content of Sump Includes Active and Anactive Regions Containment Functional Design 6.2.1-55 | |||
WATTS BAR WBNP-112 Table 6.2.1-5 Material Property Data Thermal Conductivity Volumetric Heat Material Btu/hr-ft-°F Btu/ft3-°F Paint on Steel 0.21 19.9 Paint on Concrete 0.083 39.9 Concrete 0.8 31.9 Stainless Steel 9.4 53.68 Carbon Steel 26.0 53.9 Carbon Steel* 26.0 56.4 Concrete* 0.8 28.8 Insulation on steel (containment walls)* 0.15 2.75 Insulation on steel (crane walls)* 0.20 3.663 | |||
*Located in Ice Condenser Compartment 6.2.1-56 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-6 TMD Input for Watts Bar Initial Volume PSteam PAir Temperature Element (ft3) (psia) (psia) (°F) 1 28700. 0.3 14.7 120. | |||
2 36800. | |||
3 70200. | |||
4 38800. | |||
5 36800. | |||
6 25114. | |||
25 651000. 0.3 14.7 120 26 11700. | |||
27 17900. | |||
28 11200. | |||
29 18700. | |||
30 11200. | |||
31 18000. 0.3 14.7 120. | |||
32 10100. | |||
33 15300. | |||
34 13000. | |||
35 4400. | |||
36 4400. | |||
37 9300. | |||
50 1400. | |||
0.3 14.7 120. | |||
Containment Functional Design 6.2.1-57 | |||
WATTS BAR WBNP-112 Table 6.2.1-7 TMD Flow Input Data For Watts Bar (Page 1 of 2) | |||
Flow Path Element to Flow Path Length Flow Area Loss Element (ft) (ft2) Coefficient K Area Ratio a/A 1 to 33 6.5 22 1.5 0.048 2 to 27 3.5 48 4.2 0.027 3 to 33 10.2 64 1.5 0.048 4 to 33 7.9 44 1.5 0.048 5 to 31 3.5 42 4.2 0.027 6 to 33 5.7 16 1.5 0.048 26 to 27 9.0 23 2.7 0.067 27 to 3 9.3 46 4.2 0.027 28 to 27 9.0 23 2.7 0.067 29 to 36 3.7 15 3.0 0.044 30 to 31 9.0 23 2.7 0.067 31 to 6 11.0 58 4.2 0.027 32 to 31 9.0 23 2.7 0.067 33 to 5 7.8 36 1.5 0.048 34 to 26 6.6 59 1.5 0.171 35 to 28 2.8 17 1.5 0.049 36 to 30 2.8 17 1.5 0.049 37 to 32 3.2 23 1.5 0.067 50 to 4 3.6 1.6 1.5 0.002 50 to 4 3.9 2.5 1.5 0.002 50 to 30 3.8 6.8 1.5 0.067 1 to 2 17.5 550 0.33 0.43 2 to 3 24.2 550 0.33 0.43 3 to 4 22.3 600 0.30 0.47 4 to 5 19.7 550 0.33 0.43 5 to 6 17.2 550 0.33 0.43 6 to 1 29.4 140 1.32 0.09 26 to 32 71.0 126 1.6 0.843 27 to 1 6.9 60 4.2 0.027 28 to 26 80.0 146 0.5 0.977 29 to 35 3.8 15 3.0 0.044 30 to 28 51.0 81 1.6 0.542 31 to 4 9.3 44 4.2 0.027 32 to 30 80.0 146 0.5 0.977 33 to 2 8.1 38 1.5 0.048 34 to 27 4.5 17 3.0 0.049 35 to 27 3.7 15 3.0 0.044 36 to 31 3.1 10 3.0 0.029 37 to 31 3.4 10 3.0 0.029 6.2.1-58 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-7 TMD Flow Input Data For Watts Bar (Page 2 of 2) | |||
Flow Path Element to Flow Path Length Flow Area Loss Element (ft) (ft2) Coefficient K Area Ratio a/A 40 to 1 10.36 121.9 41 to 2 10.36 144.0 42 to 3 10.36 288.0 43 to 4 10.36 199.4 44 to 5 10.36 155.1 45 to 6 10.36 155.1 Containment Functional Design 6.2.1-59 | |||
6.2.1-60 WATTS BAR Table 6.2.1-8 Calculated Maximum Peak Pressures In Lower Compartment Elements Assuming Unaugmented Flow Element 1 2 3 4 5 6 Peak Pressure (psig) 18.5 14.0 12.8 12.9 13.9 17.9 DECL - 100% Ent. | |||
Peak Pressure (psig) 16.0 12.0 10.5 10.6 12.1 15.8 DEHL - 100% Ent. | |||
Containment Functional Design WBNP-112 | |||
Containment Functional Design WATTS BAR Table 6.2.1-9 Calculated Maximum Peak Pressures In The Ice Condenser Compartment Assuming Unaugmented Flow Element 40 41 42 43 44 45 Peak Pressure (psig) 13.9 10.3 9.4 9.4 10.2 13.6 DECL - 100% Ent. | |||
Peak Pressure (psig) 11.5 8.5 7.8 7.8 8.7 11.4 DEHL - 100% Ent. | |||
6.2.1-61 WBNP-112 | |||
6.2.1-62 WATTS BAR Table 6.2.1-10 Calculated Maximum Differential Pressures Across The Operating Deck Or Lower Crane Wall Assuming Unaugmented Flow Element 1 2 3 4 5 6 Peak P (psi) 16.6 11.2 9.0 9.2 11.0 16.2 DECL - 100% Ent. | |||
Peak P (psi) 15.7 11.7 8.8 8.9 11.8 15.5 DEHL - 100% Ent. | |||
Containment Functional Design WBNP-112 | |||
Containment Functional Design WATTS BAR Table 6.2.1-11 Calculated Maximum Differential Pressures Across The Upper Crane Wall Assuming Unaugmented Flow Element 7-8-9 10-11-12 13-14-15 16-17-18 19-20-21 22-23-24 Peak P (psi) 7.2 5.9 5.6 5.7 6.0 7.2 DECL - 100% Ent. | |||
Peak P (psi) 8.4 7.1 6.4 6.3 7.01 8.4 DEHL - 100% Ent. | |||
6.2.1-63 WBNP-112 | |||
WATTS BAR WBNP-112 Table 6.2.1-12 Sensitivity Studies For D. C. Cook Plant (Page 1 of 2) | |||
CHANGE MADE CHANGE IN CHANGE IN PEAK FROM BASE OPERATING PRESSURE AGAINST PARAMETER VALUE(1) DECK P(1) THE SHELL(1) | |||
Blowdown + 10% + 11% + 12% | |||
Blowdown - 10% - 10% - 12% | |||
Blowdown - 20% - 20% - 23% | |||
Blowdown - 50% - 50% - 53% | |||
Break Compartment Inertial + 10% + 4% + 1% | |||
Length Break Compartment - 10% - 4% - 1% | |||
Inertial Length Break Compartment Volume + 10% - 2% - 1% | |||
Break Compartment Volume - 10% + 2% + 1% | |||
Break Compartment Vent Areas + 10% - 6% - 5% | |||
Break Compartment Vent Areas - 10% + 8% + 5% | |||
Door Port Failure in Break one door port fails + 1% - 1% | |||
Compartment to open Ice Mass + 10% 0 0 Ice Mass - 10% 0 0 Door Inertia + 10% + 1% 0 Door Inertia - 10% - 1% 0 All Inertial Lengths + 10% + 5% + 4% | |||
All Inertial Lengths - 10% - 5% - 3% | |||
Ice Bed Loss Coefficients + 10% 0 0 Ice Bed Loss Coefficients - 10% 0 0 Entrainment Level 0% Ent - 27% - 11% | |||
Entrainment Level 30% Ent - 19% - 15% | |||
Entrainment Level 50% Ent - 13% - 12% | |||
Entrainment Level 75% Ent - 6% - 6% | |||
Lower Compartment Loss + 10% 0 0 Coefficients Lower Compartment Loss - 10% 0 0 Coefficients Cross Flow in Lower Plenum low estimate of 0 - 7% | |||
resistance Cross Flow in Lower Plenum high estimate of 0 - 3% | |||
resistance Ice Condenser Flow Area + 10% 0 - 3% | |||
6.2.1-64 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-12 Sensitivity Studies For D. C. Cook Plant (Page 2 of 2) | |||
CHANGE MADE CHANGE IN CHANGE IN PEAK FROM BASE OPERATING PRESSURE AGAINST PARAMETER VALUE(1) DECK P(1) THE SHELL(1) | |||
Ice Condenser Flow Area - 10% 0 + 4% | |||
Ice Condenser Flow Area + 20% 0 - 6% | |||
Ice Condenser Flow Area - 20% 0 + 8% | |||
Initial Pressure in Containment + 0.3 psi + 2% + 2% | |||
Initial Pressure in Containment - 0.3 psi - 2% - 2% | |||
Initial Ice Bed Temperature + 15°F 0 0 Initial Ice Bed Temperature - 15°F 0 + 1% | |||
(1) | |||
All values shown are to the nearest percent. | |||
Containment Functional Design 6.2.1-65 | |||
WATTS BAR WBNP-112 Table 6.2.1-13 Watts Bar Ice Condenser Design Parameters Reactor Containment Volume (net free volume, ft3) | |||
Upper Compartment 692,818 Ice Compartment 110,520 Lower Compartment 273,674 Lower Compartment (dead-ended) 94,000 Total Containment Volume 1,171,012 NSSS Fraction of Nominal (FON) based on NSSS Power of, MWt 3,475* | |||
Analysis weight of ice in condenser, lbs (all main steamline 2.125x106 breaks) | |||
Core Nuclear Power - FON 100% power cases 1.006 30% power cases 0.30 0% power cases Critical at 0.0 | |||
* Includes RCP power (16 MWt) 6.2.1-66 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-14 Allowable Leakage Area For Various Reactor Coolant System Break Sizes 5 ft2 Deck Leak Resultant Peak Break Air Compression Deck Leakage Containment Pressure Size Peak (psig) Area (ft2) (psig) | |||
Double-ended 7.8 54 12.0 0.6 Double-ended 6.6 40 12.0 3 ft2 6.25 46 12.0 10 inch diameter 5.75 38 12.0 10 inch diameter* 5.75 50 10.7* | |||
6 inch diameter 5.5 41 12.0 6 inch diameter* 5.5 50 10.0* | |||
2 inch diameter 5.0 50 5.0 2 inch diameter* 4.0 50 4.2* | |||
1/2 inch diameter 3.0 >50 3.0 | |||
*This case assumes an upper compartment structural heat sink steam condensation of 6 lb/sec and 30% of deck leakage is air. | |||
Note: One spray pump at 4750 gpm at 100°F was assumed for all breaks smaller than the 3 ft2 break. | |||
Containment Functional Design 6.2.1-67 | |||
WATTS BAR WBNP-112 Table 6.2.1-15 System Parameters Initial Conditions Parameters Value Core Thermal Power (MWt) 3,411 Reactor Coolant System Flow Rate, per Loop (gpm) 93,100 Vessel Outlet Temperature (1) (°F) 619.1 (1) | |||
Core Inlet Temperature (°F) 560.6 Initial Steam Generator Steam Pressure (psia) 1,021 Steam Generator Design Model D3-2 Steam Generator Tube Plugging (%) 0 Initial Steam Generator Secondary-Side Mass (lbm) 122,474.0 Accumulator Water Volume (ft3) 1,020/tank plus 24.06 (average) per line N2 Cover Gas Pressure (psig) 585 Temperature (°F) 130 Safety Injection Delay (sec) (includes time to reach pressure 36.13 setpoint) | |||
Auxiliary Feedwater Flow (gpm/SG) 205 Notes: | |||
: 1. Analysis value includes an additional +7.0°F allowance for instrument error and dead band. | |||
6.2.1-68 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-16 Double-Ended Pump Suction Guillotine Break - Blowdown Mass and Energy Releases (Page 1 of 6) | |||
Break Side 1 (1) Break Side 2(2) | |||
Energy Energy Time Mass Thousand Mass Thousand (s) (lbm/s) (Btu/s) (lbm/s) (Btu/s) 0.0 0.0 0.0 0.0 0.0 0.001 89712.7 50762.5 43601.9 24614.6 0.1 43100.7 24412.9 22428.6 12648.0 0.2 43878.9 25045.4 24795.1 13994.7 0.3 44879.2 25882.3 24907.1 14070.4 0.4 45811.0 26740.3 24017.3 13581.4 0.5 46296.6 27360.0 22952.9 12989.7 0.6 46139.4 27584.9 21992.8 12450.9 0.7 45223.7 27319.6 21109.3 11953.3 0.8 43985.4 26824.9 20474.2 11597.1 0.9 42701.9 26278.3 20077.7 11374.8 1.0 41447.1 25735.7 19835.2 11240.1 1.1 40183.1 25190.5 19683.2 11155.2 1.2 38936.7 24657.2 19565.4 11089.2 1.3 37661.1 24105.1 19473.4 11036.9 1.4 36423.5 23568.1 19425.7 11009.6 1.5 35245.2 23054.2 19401.7 10995.8 1.6 34022.9 22492.9 19360.4 10971.9 1.7 32871.0 21946.5 19289.0 10930.6 1.8 31734.6 21380.9 19226.1 10894.3 1.9 30688.3 20849.6 19196.7 10877.7 2.0 29719.0 20347.0 19145.6 10848.7 2.1 28729.9 19813.9 19008.1 10770.4 2.2 27603.1 19171.7 18843.9 10677.2 2.3 26054.1 18218.0 18695.1 10593.3 2.4 23964.7 16858.2 18512.1 10490.0 2.5 22084.8 15634.0 18021.8 10211.8 2.6 21285.1 15167.1 17765.6 10068.3 2.7 20763.4 14860.2 17542.9 9943.5 Containment Functional Design 6.2.1-69 | |||
WATTS BAR WBNP-112 Table 6.2.1-16 Double-Ended Pump Suction Guillotine Break - Blowdown Mass and Energy Releases (Page 2 of 6) | |||
Break Side 1 (1) Break Side 2(2) | |||
Energy Energy Time Mass Thousand Mass Thousand (s) (lbm/s) (Btu/s) (lbm/s) (Btu/s) 2.8 20113.3 14438.6 17324.7 9821.2 2.9 19612.5 14118.9 17108.3 9700.2 3.0 19056.5 13752.9 16874.4 9569.2 3.1 18701.0 13528.4 16638.9 9437.3 3.2 18164.2 13168.1 16437.7 9325.3 3.3 17550.5 12755.2 16245.9 9218.7 3.4 16905.8 12316.9 16072.6 9122.6 3.5 16290.5 11894.8 15926.0 9041.9 3.6 15733.4 11509.7 15746.3 8942.1 3.7 15267.3 11186.9 15600.8 8862.1 3.8 14888.7 10922.5 15448.3 8778.0 3.9 14567.2 10694.3 15300.8 8696.8 4.0 14300.2 10503.0 15167.8 8623.9 4.2 13860.8 10179.7 14921.4 8489.1 4.4 13539.9 9932.3 14723.7 8381.9 4.6 13228.3 9681.8 15759.9 8985.3 4.8 13137.2 9570.7 15954.5 9095.2 5.0 13151.8 9527.6 15920.6 9082.5 5.2 13205.0 9523.0 15764.5 8998.2 5.4 13232.4 9509.8 15580.9 8898.7 5.6 13189.4 9458.9 15412.8 8808.0 5.8 13105.1 9387.9 15225.6 8705.9 6.0 13013.2 9317.7 15045.4 8607.1 6.2 12999.9 9298.3 14936.2 8547.9 6.4 13134.5 9349.8 14823.1 8483.5 6.6 14011.0 9906.3 14660.2 8388.9 6.8 13445.6 9484.1 14593.4 8350.5 7.0 12049.6 9046.1 14491.3 8290.2 7.2 11044.3 8594.8 14269.3 8160.8 6.2.1-70 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-16 Double-Ended Pump Suction Guillotine Break - Blowdown Mass and Energy Releases (Page 3 of 6) | |||
Break Side 1 (1) Break Side 2(2) | |||
Energy Energy Time Mass Thousand Mass Thousand (s) (lbm/s) (Btu/s) (lbm/s) (Btu/s) 7.4 11199.1 8635.2 14084.0 8055.3 7.6 11516.8 8743.9 13911.1 7958.2 7.8 11772.5 8809.3 13736.9 7858.0 8.0 12099.3 8925.1 13511.5 7727.7 8.2 12523.0 9098.9 13326.6 7621.3 8.4 12903.1 9239.2 13128.9 7507.1 8.6 13164.0 9311.3 12921.7 7387.4 8.8 13327.4 9333.9 12738.1 7281.1 9.0 13300.2 9241.2 12539.1 7165.6 9.2 13024.1 9003.5 12361.6 7062.7 9.4 12592.6 8683.4 12194.7 6965.6 9.6 12076.9 8324.0 12032.4 6871.0 9.8 11448.0 7906.1 11890.3 6788.3 10.0 10863.9 7542.2 11763.0 6714.0 10.2 10447.5 7303.8 11617.5 6629.0 10.4 10060.4 7088.1 11481.3 6550.4 10.6 9689.0 6886.9 11347.1 6473.1 10.8 9367.5 6717.4 11200.1 6388.1 11.0 9071.9 6561.8 11065.2 6310.1 11.2 8791.6 6412.8 10924.1 6228.2 11.4 8536.4 6275.7 10786.4 6148.2 11.6 8299.7 6146.7 10650.8 6069.4 11.8 8079.0 6025.4 10516.0 5991.0 12.0 7872.5 5911.3 10382.0 5913.0 12.2 7681.1 5803.5 10249.4 5836.0 12.4 7496.8 5697.1 10120.8 5761.2 12.6 7314.6 5594.3 9980.8 5679.8 12.8 7128.3 5485.9 9827.3 5591.1 13.0 6944.2 5365.6 9682.1 5507.7 Containment Functional Design 6.2.1-71 | |||
WATTS BAR WBNP-112 Table 6.2.1-16 Double-Ended Pump Suction Guillotine Break - Blowdown Mass and Energy Releases (Page 4 of 6) | |||
Break Side 1 (1) Break Side 2(2) | |||
Energy Energy Time Mass Thousand Mass Thousand (s) (lbm/s) (Btu/s) (lbm/s) (Btu/s) 13.2 6780.7 5240.7 9527.5 5418.6 13.4 6638.8 5119.2 9383.0 5335.0 13.6 6508.1 5003.2 9233.5 5248.8 13.8 6384.0 4890.9 9092.0 5167.6 14.0 6265.9 4785.1 8957.2 5090.5 14.2 6158.1 4689.5 8829.1 5017.4 14.4 6055.4 4602.3 8705.3 4947.2 14.6 5955.0 4524.1 8604.9 4891.4 14.8 5856.0 4453.3 8470.3 4815.7 15.0 5760.2 4392.0 8360.3 4755.5 15.2 5684.0 4350.0 8024.8 4580.8 15.4 5654.2 4384.9 7842.4 4529.3 15.6 5523.0 4454.8 7583.4 4416.9 15.8 5252.9 4497.7 7308.6 4275.8 16.0 4896.8 4505.0 6999.7 4065.6 16.2 4495.3 4474.7 6750.1 3833.4 16.4 4070.1 4392.0 6534.3 3584.6 16.6 3653.2 4213.2 6271.4 3301.7 16.8 3281.7 3941.6 5843.1 2955.1 17.0 2989.9 3658.9 5437.5 2650.7 17.2 2706.3 3340.7 5059.0 2385.6 17.4 2471.1 3066.5 4713.7 2156.4 17.6 2273.9 2832.7 4413.1 1964.1 17.8 2114.5 2642.0 4155.4 1805.0 18.0 1988.9 2490.7 3840.0 1631.4 18.2 1870.7 2347.3 3438.2 1425.2 18.4 1736.8 2183.1 3618.8 1451.8 18.6 1577.4 1986.1 5752.8 2254.2 18.8 1415.5 1785.4 6429.3 2514.4 6.2.1-72 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-16 Double-Ended Pump Suction Guillotine Break - Blowdown Mass and Energy Releases (Page 5 of 6) | |||
Break Side 1 (1) Break Side 2(2) | |||
Energy Energy Time Mass Thousand Mass Thousand (s) (lbm/s) (Btu/s) (lbm/s) (Btu/s) 19.0 1293.6 1635.2 5230.0 2039.3 19.2 1200.0 1519.2 3521.6 1368.4 19.4 1122.0 1422.2 3111.5 1208.0 19.6 1047.2 1328.5 2202.4 851.3 19.8 956.9 1215.0 1617.9 604.6 20.0 862.0 1095.7 2061.4 668.1 20.2 775.2 986.4 3529.8 1073.0 20.4 701.2 893.5 3910.5 1167.4 20.6 635.9 810.8 3386.7 1006.5 20.8 576.2 735.3 3000.5 889.9 21.0 529.7 676.6 2860.7 847.3 21.2 501.1 640.5 2820.9 834.8 21.4 477.5 610.8 2781.0 822.6 21.6 445.2 569.6 2667.2 788.7 21.8 408.4 522.9 2419.3 714.7 22.0 369.4 473.2 2205.5 649.5 22.2 329.3 422.2 1993.8 582.1 22.4 291.2 373.5 1777.1 512.3 22.6 252.1 323.6 1546.6 440.0 22.8 230.2 295.6 1387.1 389.4 23.0 206.7 265.6 1351.7 374.8 23.2 189.4 243.5 1379.9 380.0 23.4 173.9 223.7 1401.8 385.2 23.6 170.9 219.9 1403.5 385.8 23.8 164.1 211.2 1368.0 376.6 24.0 158.1 203.5 1257.6 347.2 24.2 151.4 194.9 1020.1 283.1 24.4 144.7 186.3 587.3 164.8 24.6 138.1 177.9 46.5 13.4 Containment Functional Design 6.2.1-73 | |||
WATTS BAR WBNP-112 Table 6.2.1-16 Double-Ended Pump Suction Guillotine Break - Blowdown Mass and Energy Releases (Page 6 of 6) | |||
Break Side 1 (1) Break Side 2(2) | |||
Energy Energy Time Mass Thousand Mass Thousand (s) (lbm/s) (Btu/s) (lbm/s) (Btu/s) 24.8 129.6 167.0 147.8 44.1 25.0 115.2 148.5 0.0 0.0 25.2 102.2 131.8 178.3 57.8 25.4 89.9 116.1 170.1 56.6 25.6 73.1 94.5 176.1 58.0 25.8 59.5 77.0 106.5 34.3 26.0 46.9 60.7 0.0 0.0 26.2 34.7 45.0 0.0 0.0 26.4 13.8 17.9 0.0 0.0 26.6 12.8 16.6 0.0 0.0 26.8 0.0 0.0 0.0 0.0 Notes: | |||
: 1. M&E exiting from the SG side of the break (path 1). | |||
: 2. M&E exiting from the pump side of the break (path 2). | |||
6.2.1-74 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-17 Double-Ended Pump Suction Guillotine Break - Reflood Mass and Energy Release - Minimum Safety Injection (Page 1 of 7) | |||
Break Side 1(1) Break Side 2(2) | |||
Time Mass Energy Mass Energy (SEC) (lbm/s) Thousand (lbm/s) Thousand (BTU/s) (BTU/s) 26.8 0.0 0.0 0.0 0.0 27.3 0.0 0.0 0.0 0.0 27.5 0.0 0.0 0.0 0.0 27.6 0.0 0.0 0.0 0.0 27.7 0.0 0.0 0.0 0.0 27.8 0.0 0.0 0.0 0.0 27.8 0.0 0.0 0.0 0.0 27.9 33.0 38.4 0.0 0.0 28.0 13.6 15.8 0.0 0.0 28.2 14.5 16.9 0.0 0.0 28.3 20.1 23.4 0.0 0.0 28.4 25.3 29.5 0.0 0.0 28.5 29.5 34.4 0.0 0.0 28.6 33.6 39.1 0.0 0.0 28.7 37.5 43.6 0.0 0.0 28.8 40.3 47.0 0.0 0.0 28.9 43.2 50.2 0.0 0.0 29.0 45.8 53.4 0.0 0.0 29.1 48.4 56.4 0.0 0.0 29.2 50.9 59.3 0.0 0.0 29.3 53.3 62.1 0.0 0.0 29.4 55.7 64.9 0.0 0.0 29.5 58.2 67.8 0.0 0.0 29.6 59.6 69.3 0.0 0.0 29.6 60.7 70.7 0.0 0.0 29.7 63.1 73.5 0.0 0.0 29.8 65.1 75.9 0.0 0.0 29.9 66.9 77.9 0.0 0.0 30.9 84.9 98.9 0.0 0.0 Containment Functional Design 6.2.1-75 | |||
WATTS BAR WBNP-112 Table 6.2.1-17 Double-Ended Pump Suction Guillotine Break - Reflood Mass and Energy Release - Minimum Safety Injection (Page 2 of 7) | |||
Break Side 1(1) Break Side 2(2) | |||
Time Mass Energy Mass Energy (SEC) (lbm/s) Thousand (lbm/s) Thousand (BTU/s) (BTU/s) 31.9 100.3 116.9 0.0 0.0 32.9 213.6 250.2 2799.9 381.2 34.0 336.1 395.6 4535.4 671.9 34.7 335.1 394.4 4521.5 673.8 35.0 333.8 392.9 4504.4 672.1 36.0 329.1 387.2 4438.4 664.3 37.0 350.1 412.4 4765.7 690.7 38.0 345.1 406.4 4698.7 682.0 39.0 340.1 400.5 4631.8 673.3 40.0 335.4 394.7 4566.1 664.6 40.5 333.0 392.0 4533.9 660.3 41.0 330.8 389.3 4502.1 656.0 42.0 326.4 384.0 4439.8 647.7 43.0 322.1 378.9 4379.5 639.7 44.0 317.4 373.3 4321.7 632.0 45.0 312.8 367.8 4265.8 624.6 46.0 308.4 362.6 4211.7 617.5 47.0 304.2 357.6 4159.4 610.5 48.0 300.2 352.8 4108.8 603.8 48.2 299.4 351.8 4098.9 602.5 49.0 296.3 348.1 4059.9 597.4 50.0 292.5 343.7 4012.4 591.1 51.0 288.9 339.4 3966.5 585.0 52.0 285.4 335.3 3921.9 579.1 53.0 282.1 331.3 3878.6 573.4 54.0 278.8 327.4 3836.7 567.9 55.0 275.7 323.7 3795.9 562.5 56.0 272.7 320.1 3756.3 557.3 57.0 269.8 316.7 3717.7 552.3 6.2.1-76 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-17 Double-Ended Pump Suction Guillotine Break - Reflood Mass and Energy Release - Minimum Safety Injection (Page 3 of 7) | |||
Break Side 1(1) Break Side 2(2) | |||
Time Mass Energy Mass Energy (SEC) (lbm/s) Thousand (lbm/s) Thousand (BTU/s) (BTU/s) 57.6 268.0 314.6 3695.1 549.3 58.0 266.9 313.3 3680.3 547.3 59.0 264.2 310.0 3643.8 542.5 60.0 261.5 306.9 3608.2 537.9 61.0 258.9 303.8 3573.6 533.3 62.0 256.4 300.9 3539.8 528.9 63.0 254.0 298.0 3506.8 524.5 64.0 251.6 295.2 3474.7 520.3 65.0 249.3 292.5 3443.3 516.2 66.0 209.2 245.0 2816.4 443.4 67.1 303.8 356.8 271.1 152.2 68.1 360.4 424.7 297.0 188.8 68.2 360.9 425.3 297.3 189.2 69.1 358.1 421.9 295.9 187.4 70.1 351.6 414.2 292.8 183.1 71.1 345.3 406.7 289.7 178.8 72.1 339.6 399.8 286.8 174.8 73.1 334.1 393.2 284.0 171.0 74.1 328.8 386.9 281.3 167.4 75.1 323.4 380.4 278.6 163.6 76.1 318.0 374.0 276.3 160.5 77.1 313.1 368.1 274.1 157.7 78.1 308.4 362.6 272.2 155.0 79.1 303.9 357.2 270.3 152.5 80.1 299.6 352.2 268.5 150.1 81.1 295.6 347.3 266.7 147.8 82.1 291.7 342.7 265.1 145.6 83.1 287.9 338.3 263.5 143.6 84.1 284.4 334.0 262.0 141.6 Containment Functional Design 6.2.1-77 | |||
WATTS BAR WBNP-112 Table 6.2.1-17 Double-Ended Pump Suction Guillotine Break - Reflood Mass and Energy Release - Minimum Safety Injection (Page 4 of 7) | |||
Break Side 1(1) Break Side 2(2) | |||
Time Mass Energy Mass Energy (SEC) (lbm/s) Thousand (lbm/s) Thousand (BTU/s) (BTU/s) 85.1 281.0 330.0 260.6 139.7 86.1 277.7 326.1 259.3 137.9 87.1 274.6 322.4 258.0 136.2 87.6 273.1 320.6 257.3 135.4 88.1 271.6 318.9 256.7 134.5 90.1 266.0 312.3 254.4 131.5 92.1 260.9 306.2 252.3 128.7 94.1 256.3 300.7 250.4 126.2 96.1 252.0 295.6 248.7 123.9 98.1 248.1 291.0 247.1 121.8 100.1 244.6 286.8 245.6 119.9 102.1 241.3 282.9 244.3 118.2 104.1 238.3 279.4 243.1 116.6 106.1 235.6 276.2 242.0 115.2 108.1 233.1 273.2 241.0 113.9 110.1 230.9 270.6 240.1 112.7 112.1 228.8 268.2 239.3 111.6 113.4 227.6 266.7 238.8 111.0 114.1 227.0 266.0 238.5 110.6 116.1 225.3 264.0 237.9 109.8 118.1 223.8 262.2 237.3 109.0 120.1 222.4 260.6 236.7 108.2 122.1 221.2 259.1 236.2 107.6 124.1 220.1 257.8 235.8 107.0 126.1 219.1 256.7 235.4 106.5 128.1 218.3 255.7 235.0 106.0 130.1 217.5 254.8 234.7 105.6 132.1 216.8 254.0 234.4 105.3 134.1 216.2 253.3 234.2 105.0 6.2.1-78 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-17 Double-Ended Pump Suction Guillotine Break - Reflood Mass and Energy Release - Minimum Safety Injection (Page 5 of 7) | |||
Break Side 1(1) Break Side 2(2) | |||
Time Mass Energy Mass Energy (SEC) (lbm/s) Thousand (lbm/s) Thousand (BTU/s) (BTU/s) 136.1 215.7 252.7 234.0 104.7 138.1 215.3 252.1 233.8 104.4 140.1 214.9 251.7 233.6 104.2 142.1 214.6 251.3 233.5 104.0 143.8 214.3 251.0 233.4 103.9 144.1 214.3 250.9 233.3 103.8 146.1 214.0 250.7 233.2 103.7 148.1 213.8 250.4 233.1 103.6 150.1 213.6 250.1 233.0 103.4 152.1 213.4 249.9 232.9 103.3 154.1 213.2 249.7 232.9 103.2 156.1 213.0 249.5 232.8 103.1 158.1 212.9 249.3 232.7 103.0 160.1 212.8 249.2 232.6 102.9 162.1 212.9 249.3 232.7 103.0 164.1 213.4 249.9 233.1 103.2 166.1 213.9 250.5 233.8 103.4 168.1 214.5 251.2 234.8 103.7 170.1 215.2 252.0 236.1 104.0 172.1 215.9 252.8 237.5 104.4 174.1 216.5 253.6 238.9 104.7 175.6 217.0 254.2 240.1 104.9 176.1 217.1 254.3 240.5 105.0 178.1 217.7 255.0 242.1 105.3 180.1 218.1 255.5 243.6 105.5 182.1 218.5 255.9 245.2 105.7 184.1 218.8 256.3 246.8 105.9 186.1 219.0 256.6 248.4 106.0 188.1 219.2 256.8 250.1 106.1 Containment Functional Design 6.2.1-79 | |||
WATTS BAR WBNP-112 Table 6.2.1-17 Double-Ended Pump Suction Guillotine Break - Reflood Mass and Energy Release - Minimum Safety Injection (Page 6 of 7) | |||
Break Side 1(1) Break Side 2(2) | |||
Time Mass Energy Mass Energy (SEC) (lbm/s) Thousand (lbm/s) Thousand (BTU/s) (BTU/s) 190.1 219.3 256.9 251.8 106.2 192.1 219.4 257.0 253.5 106.3 194.1 219.4 257.0 255.3 106.4 196.1 219.3 256.9 257.1 106.4 198.1 219.2 256.8 258.9 106.4 200.1 219.0 256.5 260.8 106.4 202.1 218.7 256.2 262.7 106.3 204.1 218.4 255.9 264.6 106.3 206.1 218.0 255.4 266.6 106.2 207.0 217.8 255.2 267.5 106.2 208.1 217.6 254.9 268.5 106.1 210.1 217.1 254.3 270.6 106.0 212.1 216.6 253.6 272.7 105.9 214.1 216.0 253.0 274.8 105.8 216.1 215.4 252.3 277.0 105.6 218.1 214.7 251.5 279.3 105.5 220.1 214.0 250.7 281.7 105.4 222.1 213.2 249.7 284.0 105.2 224.1 212.4 248.7 286.4 105.1 226.1 211.5 247.6 288.8 104.9 228.1 210.5 246.5 291.2 104.7 230.1 209.5 245.3 293.7 104.5 6.2.1-80 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-17 Double-Ended Pump Suction Guillotine Break - Reflood Mass and Energy Release - Minimum Safety Injection (Page 7 of 7) | |||
Break Side 1(1) Break Side 2(2) | |||
Time Mass Energy Mass Energy (SEC) (lbm/s) Thousand (lbm/s) Thousand (BTU/s) (BTU/s) 232.1 208.4 244.0 296.1 104.3 234.1 207.2 242.6 298.5 104.1 236.1 206.0 241.1 300.8 103.8 238.1 204.7 239.6 303.2 103.6 239.8 203.5 238.3 305.3 103.4 Notes: | |||
: 1. M&E exiting from the SG side of the break (path 1). | |||
: 2. M&E exiting from the pump side of the break (path 2). | |||
Containment Functional Design 6.2.1-81 | |||
6.2.1-82 WATTS BAR Table 6.2.1-18 Double-Ended Pump Suction Guillotine Break - Minimum Safety Injection Principal Parameters During Reflood (Page 1 of 2) | |||
Flooding Flooding Core Total Time Temp Rate Carryover Height Downcomer Flow Injection Accumulator Spill Enthalpy (sec) (Deg-F) (in/s) Fraction (ft) Height (ft) Fraction (lbm/sec) (lbm/sec) (lbm/sec) (btu/lbm) 26.8 205.9 0.00 0.00 0.00 0.00 0.25 0.00 0.0 0.0 0.00 27.6 203.1 22.33 0.00 0.66 1.45 0.00 7357.70 7357.7 0.0 99.46 27.8 201.6 24.19 0.00 1.04 1.37 0.00 7305.50 7305.5 0.0 99.46 28.2 201.0 2.35 0.10 1.30 2.16 0.24 7176.60 7176.6 0.0 99.46 28.4 201.0 2.39 0.14 1.34 2.85 0.29 7122.10 7122.1 0.0 99.46 29.6 201.3 2.04 0.33 1.50 6.35 0.35 6851.00 6851.0 0.0 99.46 30.9 201.8 1.98 0.46 1.64 10.39 0.37 6577.20 6577.2 0.0 99.46 34.0 202.7 3.73 0.62 1.93 16.12 0.57 5416.30 5416.3 0.0 99.46 34.7 202.8 3.58 0.64 2.01 16.12 0.57 5311.60 5311.6 0.0 99.46 35.0 202.9 3.52 0.65 2.04 16.12 0.57 5273.40 5273.4 0.0 99.46 36.0 203.2 3.36 0.68 2.13 16.12 0.57 5155.20 5155.2 0.0 99.46 37.0 203.6 3.44 0.69 2.23 16.12 0.58 5495.40 4908.2 0.0 96.64 40.5 205.1 3.15 0.72 2.51 16.12 0.57 5177.60 4584.7 0.0 96.44 Containment Functional Design 48.2 209.2 2.78 0.75 3.00 16.12 0.56 4645.90 4044.6 0.0 96.04 57.6 215.0 2.50 0.76 3.50 16.12 0.55 4174.10 3566.0 0.0 95.62 66.0 220.5 2.07 0.77 3.90 16.12 0.51 3193.60 2573.8 0.0 94.34 WBNP-112 67.1 221.1 2.75 0.77 3.94 16.11 0.59 603.00 0.0 0.0 73.06 68.2 221.8 3.10 0.76 4.00 15.96 0.60 581.20 0.0 0.0 73.06 | |||
Table 6.2.1-18 Double-Ended Pump Suction Guillotine Break - Minimum Safety Injection Principal Parameters During Reflood Containment Functional Design WATTS BAR (Page 2 of 2) | |||
Flooding Flooding Core Total Time Temp Rate Carryover Height Downcomer Flow Injection Accumulator Spill Enthalpy (sec) (Deg-F) (in/s) Fraction (ft) Height (ft) Fraction (lbm/sec) (lbm/sec) (lbm/sec) (btu/lbm) 77.1 227.1 2.67 0.77 4.51 14.90 0.60 596.30 0.0 0.0 73.06 87.6 232.2 2.35 0.78 5.00 14.24 0.59 605.00 0.0 0.0 73.06 100.1 237.0 2.11 0.78 5.51 13.94 0.58 610.80 0.0 0.0 73.06 113.4 241.1 1.97 0.79 6.00 13.97 0.58 614.10 0.0 0.0 73.06 130.1 245.3 1.88 0.79 6.56 14.26 0.57 616.00 0.0 0.0 73.06 143.8 247.5 1.85 0.80 7.00 14.62 0.57 616.60 0.0 0.0 73.06 160.1 246.7 1.84 0.80 7.51 15.09 0.57 616.90 0.0 0.0 73.06 175.6 247.5 1.86 0.80 8.00 15.50 0.58 616.20 0.0 0.0 73.06 186.1 247.0 1.87 0.79 8.34 15.71 0.58 615.80 0.0 0.0 73.06 192.1 247.2 1.86 0.79 8.53 15.80 0.58 615.70 0.0 0.0 73.06 207.0 247.3 1.84 0.79 9.00 15.96 0.58 615.90 0.0 0.0 73.06 224.1 247.5 1.78 0.79 9.53 16.07 0.59 616.70 0.0 0.0 73.06 239.8 247.3 1.70 0.79 10.00 16.11 0.59 618.10 0.0 0.0 73.06 6.2.1-83 WBNP-112 | |||
WATTS BAR WBNP-112 Table 6.2.1-19 Double-Ended Pump Suction Guillotine Break - Post-Reflood Mass and Energy Releases - Minimum Safety Injection (Page 1 of 3) | |||
Break Side 1(1) Break Side 2(2) | |||
Mass Energy Mass Energy Time (lbm/s) Thousand (lbm/s) Thousand (SEC) (BTU/s) (BTU/s) 239.8 210.0 263.1 427.2 118.0 244.8 209.2 262.1 428.0 118.1 249.8 209.7 262.8 427.4 117.9 254.8 208.9 261.8 428.2 117.9 259.8 208.1 260.7 429.1 118.0 264.8 208.6 261.4 428.5 117.8 269.8 207.8 260.3 429.4 117.8 274.8 208.3 260.9 428.9 117.6 279.8 207.4 259.9 429.8 117.7 284.8 206.5 258.8 430.6 117.8 289.8 207.0 259.3 430.2 117.6 294.8 206.1 258.2 431.1 117.7 299.8 206.5 258.7 430.7 117.5 304.8 205.6 257.6 431.6 117.6 309.8 206.0 258.0 431.2 117.4 314.8 205.0 256.9 432.1 117.5 319.8 205.4 257.3 431.8 117.3 324.8 204.4 256.1 432.8 117.4 329.8 204.7 256.5 432.5 117.2 334.8 203.7 255.3 433.4 117.3 339.8 204.0 255.6 433.2 117.1 344.8 203.0 254.3 434.2 117.2 349.8 203.2 254.6 434.0 117.1 354.8 202.2 253.3 435.0 117.2 359.8 202.3 253.5 434.8 117.0 364.8 201.3 252.2 435.9 117.2 369.8 201.4 252.4 435.8 117.0 374.8 201.5 252.5 435.7 116.9 379.8 200.4 251.1 436.8 117.0 6.2.1-84 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-19 Double-Ended Pump Suction Guillotine Break - Post-Reflood Mass and Energy Releases - Minimum Safety Injection (Page 2 of 3) | |||
Break Side 1(1) Break Side 2(2) | |||
Mass Energy Mass Energy Time (lbm/s) Thousand (lbm/s) Thousand (SEC) (BTU/s) (BTU/s) 384.8 200.4 251.1 436.7 116.9 389.8 200.5 251.2 436.7 116.8 394.8 199.3 249.7 437.9 116.9 399.8 199.3 249.7 437.9 116.8 404.8 199.3 249.7 437.8 116.7 409.8 199.3 249.8 437.8 116.6 414.8 198.2 248.4 438.9 116.7 419.8 198.2 248.3 439.0 116.6 424.8 198.1 248.2 439.0 116.5 429.8 198.0 248.1 439.1 116.4 434.8 196.8 246.6 440.4 116.6 439.8 196.6 246.4 440.5 116.5 444.8 196.4 246.1 440.8 116.5 449.8 196.1 245.8 441.0 116.4 454.8 195.8 245.4 441.3 116.4 459.8 195.5 244.9 441.7 116.3 464.8 195.1 244.4 442.1 116.3 469.8 194.6 243.9 442.5 116.3 474.8 194.1 243.2 443.0 116.3 479.8 194.5 243.7 442.6 116.1 484.8 193.9 242.9 443.3 116.2 489.8 193.2 242.1 444.0 116.2 494.8 193.4 242.3 443.8 116.1 499.8 192.5 241.2 444.7 116.1 504.8 192.5 241.2 444.7 116.0 509.8 192.3 241.0 444.8 115.9 514.8 192.1 240.7 445.1 115.9 519.8 191.7 240.2 445.4 115.9 524.8 191.2 239.6 446.0 115.9 Containment Functional Design 6.2.1-85 | |||
WATTS BAR WBNP-112 Table 6.2.1-19 Double-Ended Pump Suction Guillotine Break - Post-Reflood Mass and Energy Releases - Minimum Safety Injection (Page 3 of 3) | |||
Break Side 1(1) Break Side 2(2) | |||
Mass Energy Mass Energy Time (lbm/s) Thousand (lbm/s) Thousand (SEC) (BTU/s) (BTU/s) 529.8 190.5 238.7 446.6 115.9 534.8 190.5 238.7 446.6 115.8 539.8 190.3 238.5 446.8 115.7 544.8 189.9 237.9 447.3 115.7 549.8 189.2 237.0 448.0 115.8 554.8 188.9 236.7 448.2 115.7 559.8 188.3 236.0 448.8 115.7 564.8 188.0 235.6 449.1 115.7 569.8 187.9 235.4 449.3 115.6 574.8 187.6 235.1 449.5 115.5 579.8 187.2 234.5 450.0 115.5 584.8 186.7 234.0 450.4 115.5 589.8 186.4 233.5 450.8 115.5 594.8 186.0 233.1 451.1 115.4 599.8 185.6 232.6 451.5 115.4 910.7 185.6 232.6 451.5 115.4 910.8 75.2 94.0 562.0 138.6 914.8 75.1 93.9 562.1 138.5 1204.8 70.2 87.8 566.9 137.5 1207.3 70.2 87.7 566.9 137.4 1262.3 69.4 86.7 567.7 135.7 1267.3 69.3 86.6 573.1 150.7 1342.3 68.2 85.2 574.2 148.4 1344.3 68.1 85.1 356.3 127.4 2267.2 68.1 85.1 356.3 127.4 Notes: | |||
: 1. M&E exiting from the SG side of the break (path 1). | |||
: 2. M&E exiting from the pump side of the break (path 2). | |||
6.2.1-86 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-20 Decay Heat Curve (Page 1 of 2) | |||
TIME (Sec) Decay Heat (P/Po) | |||
: 10. .0506850 | |||
: 15. 0.477187 | |||
: 20. .0456218 | |||
: 40. .0406962 | |||
: 60. .0378482 | |||
: 80. .0358667 100. .0343802 150. .0318330 200. .0301404 400. .0264229 600. .0242907 800. .0227336 1000. .0214999 1500. .0192069 2000. .0175824 4000. .0140451 6000. .0123786 8000. .0113975 10000. .0107264 15000. .0100411 20000. .0093567 40000. .0079090 60000. .0071368 80000. .0066021 100000. .0062046 150000. .0054924 200000. .0050014 400000. .0038711 600000. .0032712 800000. .0028872 1000000. .0026231 1500000. .0022001 Containment Functional Design 6.2.1-87 | |||
WATTS BAR WBNP-112 Table 6.2.1-20 Decay Heat Curve (Page 2 of 2) | |||
TIME (Sec) Decay Heat (P/Po) 2000000. .0019386 4000000. .0013911 6000000. .0011338 8000000. .0009754 10000000. .0008662 6.2.1-88 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-21 Deleted By Amendment 97 Containment Functional Design 6.2.1-89 | |||
WATTS BAR WBNP-112 Table 6.2.1-22 Deleted By Amendment 97 6.2.1-90 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 1 of 10) | |||
Time Mass Flow Energy Flow Avg. Enthalpy (sec) (lbm/sec) (Btu/sec) (Btu/lbm) 0.00000 9.6110000E+03 5.3946543E+06 561.30 0.00101 4.3310502E+04 2.4100795E+07 556.47 0.00201 5.6464849E+04 3.1421870E+07 556.49 0.00301 6.1520189E+04 3.4231211E+07 556.42 0.00401 6.2907110E+04 3.4995181E+07 556.30 0.00501 6.2527557E+04 3.4773203E+07 556.13 0.00601 6.1359842E+04 3.4111223E+07 555.92 0.00701 5.9847065E+04 3.3257665E+07 555.71 0.00801 5.8188878E+04 3.2325854E+07 555.53 0.00900 5.6669717E+04 3.1475995E+07 555.43 0.01001 5.5334196E+04 3.0733067E+07 555.41 0.01101 5.4380116E+04 3.0206926E+07 555.48 0.01202 5.3848579E+04 2.9918413E+07 555.60 0.01301 5.3722982E+04 2.9856042E+07 555.74 0.01403 5.3913587E+04 2.9968612E+07 555.86 0.01503 5.4272426E+04 3.0172312E+07 555.94 0.01602 5.4632246E+04 3.0374580E+07 555.98 0.01700 5.4934445E+04 3.0543650E+07 556.00 0.01803 5.5232000E+04 3.0709908E+07 556.02 0.01903 5.5482063E+04 3.0849637E+07 556.03 0.02004 5.5707346E+04 3.0975819E+07 556.05 0.02101 5.5896536E+04 3.1082274E+07 556.07 0.02205 5.6078108E+04 3.1185010E+07 556.10 0.02300 5.6240106E+04 3.1277094E+07 556.14 0.02402 5.6414116E+04 3.1376145E+07 556.18 0.02504 5.6591029E+04 3.1476717E+07 556.21 0.02606 5.6764048E+04 3.1574969E+07 556.25 0.02702 5.6928226E+04 3.1668125E+07 556.28 0.02806 5.7102526E+04 3.1766906E+07 556.31 0.02902 5.7263203E+04 3.1857866E+07 556.34 0.03003 5.7428068E+04 3.1951113E+07 556.37 0.03101 5.7583531E+04 3.2038998E+07 556.39 0.03202 5.7746706E+04 3.2131054E+07 556.41 0.03304 5.7903222E+04 3.2219280E+07 556.43 0.03401 5.8052067E+04 3.2303155E+07 556.45 0.03501 5.8195321E+04 3.2383957E+07 556.47 0.03601 5.8331171E+04 3.2460804E+07 556.49 0.03703 5.8470775E+04 3.2540002E+07 556.52 0.03801 5.8606356E+04 3.2616877E+07 556.54 Containment Functional Design 6.2.1-91 | |||
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 2 of 10) 04012 5.8872406E+04 3.2768324E+07 556.60 | |||
.04101 5.9008660E+04 3.2846908E+07 556.65 | |||
.04201 5.9153822E+04 3.2932609E+07 556.73 | |||
.04300 5.9313778E+04 3.302664 E+07 556.81 | |||
.04401 5.9490981E+04 3.3130077E+07 556.89 | |||
.04501 5.9679056E+04 3.3239170E+07 556.97 | |||
.04600 5.9873576E+04 3.3351437E+07 557.03 | |||
.04700 6.0077022E+04 3.3468342E+07 557.09 | |||
.04800 6.0407806E+04 3.3677849E+07 557.51 | |||
.04900 6.0986562E+04 3.4009096E+07 557.65 | |||
.05000 6.1649802E+04 3.4384106E+07 557.73 | |||
.05100 6.2310578E+04 3.4754624E+07 557.76 | |||
.05200 6.2917709E+04 3.5094556E+07 557.79 | |||
.05302 6.3477117E+04 3.5407841E+07 557.80 | |||
.05401 8.3423661E+04 4.6840941E+07 561.48 | |||
.05501 7.3060968E+04 4.3557140E+07 557.99 | |||
.05601 8.0518030E+04 4.5030731E+07 559.26 | |||
.05700 8.2563578E+04 4.6098557E+07 558.34 | |||
.05800 8.3815137E+04 4.6812762E+07 558.52 | |||
.05902 8.3449231E+04 4.6592537E+07 558.33 | |||
.06000 8.4269954E+04 4.7056412E+07 558.40 | |||
.06101 8.4735994E+04 4.7306624E+07 558.28 | |||
.06202 8.3970123E+04 4.6856778E+07 558.02 | |||
.06300 8.4285244E+04 4.6484834E+07 558.14 | |||
.06403 8.4394816E+04 4.7109317E+07 558.20 | |||
.06502 8.4573828E+04 4.7202661E+07 558.12 | |||
.06611 8.4787755E+04 4.7325979E+07 558.17 | |||
.06703 8.5532633E+04 4.7747200E+07 558.23 | |||
.06802 8.5992772E+04 4.8003061E+07 558.22 | |||
.06902 8.5421297E+04 4.8244326E+07 558.25 | |||
.07004 8.5727778E+04 4.8412801E+07 558.22 | |||
.07102 8.6796001E+04 4.8448914E+07 558.19 | |||
.07203 8.6870937E+04 4.8490730E+07 558.19 | |||
.07304 8.7054880E+04 4.8594295E+07 558.20 | |||
.07402 8.7178558E+04 4.8661343E+07 558.18 | |||
.07501 8.7144334E+04 4.8640448E+07 558.16 | |||
.07605 8.7239117E+04 4.8595232E+07 558.18 | |||
.07706 8.7495940E+04 4.8840764E+07 558.21 | |||
.07803 8.7779389E+04 4.9001329E+07 558.23 | |||
.07905 8.8111858E+04 4.9189719E+07 558.26 | |||
.08014 8.8437477E+04 4.9373735E+07 558.29 6.2.1-92 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 3 of 10) | |||
.08101 8.8713080E+04 4.9529214E+07 558.31 | |||
.08237 8.8970751E+04 4.9673906E+07 558.32 | |||
.08339 9.9150300E+04 4.9774884E+07 558.32 | |||
.08404 9.9278550E+04 4.9845700E+07 558.32 | |||
.08701 8.9412638E+04 5.01462878+07 558.34 | |||
.08800 9.0027554E+04 5.0267688E+07 556.36 | |||
.08903 9.0281189E+04 5.0411020E+07 557.36 | |||
.09005 9.0539626E+04 5.0556703E+07 557.39 | |||
.09101 9.0743822E+04 5.0671166E+07 557.40 | |||
.09207 9.0000901E+04 5.0758235E+07 557.39 | |||
.09305 9.0086401E+04 5.0804912E+07 557.38 | |||
.09412 9.1143158E+04 5.8835575E+07 557.37 | |||
.09510 9.1106623E+04 5.0870216E+07 557.36 | |||
.09608 9.1186559E+04 5.0914656E+07 557.36 | |||
.09708 9.1302596E+04 5.0979666E+07 561.36 | |||
.09806 9.1443286E+04 5.1058782E+07 557.37 | |||
.09903 9.1592551E+04 5.1142472E+07 559.37 | |||
.19006 9.1728833E+04 5.1218292E+07 558.37 | |||
.19514 9.2351448E+04 5.1394011E+07 558.32 | |||
.11012 9.2387798E+04 5.1578304E+07 558.28 | |||
.11511 9.2236260E+04 5.1486172E+07 558.20 | |||
.12001 9.2917771E+04 5.1359571E+07 558.15 | |||
.12514 9.1727154E+04 5.1196412E+07 558.14 | |||
.13014 9.1623195E+04 5.1144798E+07 558.21 | |||
.13511 9.1748740E+04 5.1225781E+07 558.33 | |||
.14004 9.2120808E+04 5.1446366E+07 558.47 | |||
.14512 9.2579812E+04 5.1712621E+07 558.57 | |||
.15007 9.2941215E+04 5.1919892E+07 558.63 | |||
.15519 9.3225048E+04 5.2081879E+07 558.67 | |||
.16003 9.3491097E+04 5.2233133E+07 558.70 | |||
.16505 9.3818313E+04 5.24190993+07 558.73 | |||
.17002 9.4199119E+04 5.2634778E+07 558.76 | |||
.17500 9.4556660E+04 5.2836777E+07 558.78 | |||
.18010 9.4834408E+04 5.2992611E+07 558.79 | |||
.18509 9.4979093E+04 5.3072559E+07 558.78 | |||
.19007 9.4971100E+04 5.3065115E+07 558.75 | |||
.19508 9.4787975E+04 5.2958276E+07 558.70 | |||
.20001 9.4482682E+04 5.2783541E+07 558.66 | |||
.21003 9.3857870E+04 5.2426175E+07 558.57 | |||
.22004 9.3482892E+04 5.2212471E+07 558.52 | |||
.23008 9.3115899E+04 5.2007458E+07 558.52 | |||
.24014 9.2880327E+04 5.1879691E+07 558.56 Containment Functional Design 6.2.1-93 | |||
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 4 of 10) 25011 9.2987393E+04 5.1899210E+07 558.61 | |||
.26085 9.3088912E+04 5.2004007E+07 558.65 | |||
.27007 9.3293866E+04 5.2120524E+07 558.67 | |||
.28013 9.3546973E+04 5.2264903E+07 558.70 | |||
.29015 8.3725635E+04 5.2365366E+07 558.71 | |||
.30009 9.3670696E+04 5.2332535E+07 558.69 | |||
.31008 9.3507989E+04 5.2239258E+07 558.66 5.2040402E+07 558.62 | |||
.34021 9.2638976E+04 5.1748157E+07 558.60 | |||
.35012 9.2708694E+04 5.1789509E+07 558.63 | |||
.36001 9.2722621E+04 5.1797589E+07 558.63 | |||
.37009 9.2570379E+04 5.1711187E+07 558.61 | |||
.38006 9.2414695E+04 5.1623414E+07 558.61 | |||
.39010 9.2271423E+04 5.1542499E+07 558.60 | |||
.40010 9.2084414E+04 5.1436520E+07 558.58 | |||
.41010 9.1843519E+04 5.1300115E+07 558.56 | |||
.42012 9.1577114E+04 5.1149514E+07 558.54 | |||
.43000 9.1310985E+04 5.0999398E+07 558.52 | |||
.44012 9.1118166E+04 5.0891429E+07 558.52 | |||
.45008 9.1177214E+04 5.0987004E+07 558.54 | |||
.46010 9.1130754E+04 5.0901754E+07 558.56 | |||
.47012 9.1171899E+04 5.0925777E+07 558.57 | |||
.48011 9.1141485E+04 5.0908756E+07 558.57 | |||
.49018 9.1030159E+04 5.0845649E+07 558.56 | |||
.50000 9.0877513E+04 5.0759274E+07 558.55 | |||
.51009 9.0716741E+04 5.0668508E+07 558.54 | |||
.52016 9.0525631E+04 5.0550518E+07 558.52 | |||
.53004 9.0280616E+04 5.0422042E+07 558.50 | |||
.54012 9.0027339E+04 5.0279431E+07 558.49 | |||
.55066 9.9853472E+04 5.0182236E+07 558.49 | |||
.56012 9.9756392E+04 5.0128690E+07 558.50 | |||
.57015 9.9702675E+04 5.0099544E+07 558.51 | |||
.58001 9.9656269E+04 5.0074286E+07 558.51 | |||
.59012 9.9574430E+04 5.0028693E+07 558.52 | |||
.60022 9.9437753E+04 4.9951947E+07 558.51 | |||
.61017 9.9276720E+04 4.9861529E+07 558.51 | |||
.62017 9.9112503E+04 4.9769422E+07 558.50 | |||
.63018 9.8927891E+04 4.9665729E+07 558.49 | |||
.64017 9.8714678E+04 4.9545884E+07 558.49 | |||
.65015 9.3497653E+04 4.9424142E+07 558.48 | |||
.66017 9.8310815E+04 4.9319743E+07 558.48 | |||
.67013 9.8164091E+04 4.9238154E+07 558.48 | |||
.68016 9.8043186E+04 4.9171145E+07 558.49 6.2.1-94 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 5 of 10) 69053 8.7936650E+04 4.9112289E+07 558.50 | |||
.70013 8.7833343E+04 4.9055160E+07 558.50 | |||
.71015 8.7699937E+04 4.8980863E+07 558.51 | |||
.72002 8.7515577E+04 4.8877576E+07 558.50 | |||
.73008 8.7289861E+04 4.8751064E+07 558.50 | |||
.74014 8.7057520E+04 4.8620990E+07 558.49 | |||
.75005 8.6822139E+04 4.8489298E+07 558.49 | |||
.76008 8.6586328E+04 4.8357560E+07 558.49 | |||
.77012 8.6371277E+14 4.8237750E+07 558.49 | |||
.78012 8.6187553E+04 4.8135776E+07 558.50 | |||
.81011 8.5732780E+04 4.7883581E+07 558.52 | |||
.82014 8.5520138E+04 4.7765060E+07 558.52 | |||
.83011 8.5279840E+04 4.7631116E+07 558.53 | |||
.84001 8.5205251E+04 4.7592350E+07 558.56 | |||
.85012 8.5219901E+04 4.7603442E+07 558.60 | |||
.85617 8.5236961E+04 4.7615294E+07 558.62 | |||
.87004 8.5239912E+04 4.7613376E+07 558.65 | |||
.88005 8.5224810E+04 4.7612265E+07 558.67 | |||
.89012 8.5153610E+04 4.7573612E+07 558.68 | |||
.90013 8.5034214E+04 4.7507903E+07 558.69 | |||
.91018 8.4921660E+04 4.7446462E+07 558.71 | |||
.92003 8.4789254E+04 4.7373665E+07 558.72 | |||
.93003 8.4585424E+04 4.7260284E+07 558.73 | |||
.94006 8.4332775E+04 4.7119694E+07 558.73 | |||
.95004 8.4133386E+04 4.7009576E+07 558.75 | |||
.96805 8.4001069E+04 4.6937622E+07 558.77 | |||
.97019 8.3879090E+04 4.6871592E+07 558.80 | |||
.98017 8.3749242E+04 4.6801373E+07 558.83 | |||
.99016 8.3650306E+04 4.6748791E+07 558.86 1.00013 8.3577220E+04 4.6710517E+07 558.89 1.01003 8.3483239E+04 4.6660040E+07 558.92 1.02009 8.3363850E+04 4.6595179E+07 558.94 1.03008 8.3228098E+04 4.6521139E+07 558.96 1.04013 8.3054020E+04 4.6425558E+07 558.98 1.05007 8.2852281E+04 4.6314604E+07 559.00 1.06002 8.2670415E+04 4.6215242E+07 559.03 1.07002 8.2522495E+04 4.6135141E+07 559.06 1.08015 8.2370134E+04 4.6052391E+07 559.09 1.09014 8.2204789E+04 4.5962487E+07 559.12 1.10008 8.2058899E+04 4.5883869E+07 559.16 1.11016 8.1925541E+04 4.5812566E+07 559.20 1.12013 8.1778838E+04 4.5733459E+07 559.23 1.13009 8.1614966E+04 4.5644519E+07 559.27 Containment Functional Design 6.2.1-95 | |||
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 6 of 10) 1.14014 8.1440550E+04 4.5549601E+07 559.30 1.15001 8.1233556E+04 4.5436190E+07 559.33 1.16016 8.0973459E+04 4.5290008E+07 559.36 1.17009 8.0728542E+04 4.5158681E+07 559.39 1.18005 8.0505981E+04 4.5037156E+07 559.43 1.19012 8.0276950E+04 4.4911852E+07 559.46 1.20014 8.0035318E+04 4.4779364E+07 559.50 1.21009 7.9809170E+04 4.4655876E+07 559.53 1.22016 7.9592878E+14 4.4537896E+07 559.57 1.23000 7.9352507E+04 4.4406088E+07 559.61 1.24005 7.9096790E+04 4.4266220E+07 559.65 1.25005 7.8854282E+04 4.4133853E+07 559.69 1.28004 7.8874567E+04 4.3707164E+07 559.81 1.29005 7.7872559E+04 4.3597579E+07 559.86 1.31002 7.7659289E+04 4.3481315E+07 559.90 1.31001 7.7437311E+04 4.3359385E+07 559.93 1.32002 7.7200854E+04 4.3229663E+07 559.96 1.33004 7.6991619E+04 4.3115571E+07 560.00 1.34011 7.6778950E+04 4.2999371E+07 560.04 1.35008 7.6585125E+04 4.2893425E+07 560.07 1.36005 7.6481499E+04 4.2793469E+07 560.11 1.37017 7.6219116E+04 4.2694227E+07 560.15 1.38018 7.6034026E+04 4.2593341E+07 560.19 1.39004 7.5849854E+04 4.2492871E+07 560.22 1.40005 7.5667828E+04 4.2393603E+07 560.26 1.41010 7.5482159E+04 4.2292249E+07 560.29 1.42010 7.5301664E+04 4.2193864E+07 560.33 1.43011 7.6139111E+04 4.2105856E+07 560.37 1.44001 7.5009647E+04 4.2036718E+07 560.42 1.45008 7.4931627E+04 4.1196682E+07 560.47 1.46010 7.4867239E+04 4.1963757E+07 560.51 1.47017 7.4753854E+04 4.1902791E+07 560.54 1.48013 7.4584355E+04 4.1810194E+07 560.58 1.49012 7.4392609E+04 4.1705259E+07 560.61 1.50012 7.4197644E+04 4.1598646E+07 560.65 1.51013 7.4006729E+04 4.1494259E+07 560.68 1.52018 7.3815196E+04 4.1389571E+07 560.72 1.53011 7.3936081E+04 4.1291938E+07 560.76 1.54014 7.3469148E+04 4.1201423E+07 560.80 1.55011 7.3320510E+04 4.1121431E+07 560.84 1.56014 7.3181275E+04 4.1046863E+07 560.89 1.57010 7.3026251E+04 4.0963136E+07 560.94 1.58010 7.2837043E+04 4.0859867E+07 560.98 6.2.1-96 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 7 of 10) 1.59014 7.2631221E+04 4.0747358E+07 561.02 1.61016 7.2432964E+04 4.0639399E+07 561.06 1.61016 7.2278283E+04 4.0556143E+07 561.11 1.62016 7.2205320E+04 4.0519020E+07 561.16 1.63013 7.2141973E+04 4.0487008E+07 561.21 1.64018 7.2049835E+04 4.0438786E+07 561.26 1.65012 7.1952016E+04 4.0387622E+07 561.31 1.66000 7.1844712E+04 4.0331199E+07 561.37 1.67014 7.1713907E+14 4.0261546E+07 561.42 1.68057 7.1575164E+04 4.0187249E+07 561.47 1.69009 7.1433733E+04 4.0111463E+07 561.52 1.70017 7.1277095E+04 4.0027105E+07 561.57 1.71018 7.1122032E+04 3.9943672E+07 561.62 1.75021 7.0507943E+04 3.9613307E+07 561.83 1.76009 7.0358714E+04 3.9533318E+07 561.88 1.77019 7.0222660E+04 3.9460948E+07 561.94 1.78019 7.0103256E+04 3.9398041E+07 562.00 1.79014 7.0001645E+04 3.9345011E+07 562.12 1.80016 6.9902190E+04 3.9293287E+07 562.18 1.81014 6.9809830E+04 3.9245446E+07 562.24 1.82015 6.9723055E+04 3.9200754E+07 562.29 1.83015 6.9630793E+04 3.9152920E+07 562.35 1.84003 6.9530524E+04 3.9100463E+07 562.41 1.85001 6.9432184E+04 3.9049105E+07 562.47 1.86011 6.9343257E+04 3.9003180E+07 562.52 1.87003 6.9260802E+04 3.8960691E+07 562.58 1.88007 6.9176562E+04 3.8917304E+07 562.63 1.89010 6.9092618E+04 3.8873771E+07 562.69 1.90007 6.9003582E+04 3.8827388E+07 562.74 1.91019 6.8908110E+04 3.8777285E+07 562.79 1.92010 6.8805926E+04 3.8723321E+07 562.84 1.93016 6.8697856E+04 3.8665875E+07 562.89 1.94013 6.8580875E+04 3.8603405E+07 562.94 1.95012 6.8467934E+04 3.8543229E+07 562.99 1.96015 6.8363888E+04 3.8488157E+07 563.04 1.97008 6.8266519E+04 3.8436705E+07 563.09 1.98019 6.8166411E+04 3.8383543E+07 563.13 1.99010 6.8062479E+04 3.8328037E+07 563.17 2.00009 6.7955066E+04 3.8270409E+07 563.21 2.01004 6.7847138E+04 3.8212316E+07 563.25 2.02017 6.7766440E+04 3.8169703E+07 563.29 2.03017 6.7709804E+04 3.8140337E+07 563.33 2.04017 6.7640349E+04 3.8103566E+07 563.36 Containment Functional Design 6.2.1-97 | |||
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 8 of 10) 2.05012 6.7567787E+04 3.8064924E+07 563.36 2.06017 6.7489652E+04 3.8023025E+07 563.39 2.07014 6.7395491E+04 3.7971956E+07 563.42 2.08012 6.7294517E+04 3.7916962E+07 563.45 2.09012 6.7180594E+04 3.7854570E+07 563.47 2.10000 6.7053291E+04 3.7784487E+07 563.50 2.11005 6.6918837E+04 3.7710383E+07 563.52 2.12005 6.6783490E+04 3.7635639E+07 563.55 2.13015 6.6634430E+04 3.7553098E+07 563.57 2.14013 6.6483182E+04 3.7469266E+07 563.59 2.15015 6.6334740E+04 3.7386995E+07 563.61 2.16011 6.6191907E+04 3.7307832E+07 563.63 2.17006 6.6059863E+04 3.7234710E+07 563.65 2.18002 6.5933205E+04 3.7164554E+07 563.67 2.22006 6.5472840E+04 3.6909501E+07 563.74 2.23010 6.5360076E+04 3.6847037E+07 563.75 2.24010 6.5251847E+04 3.6787039E+07 563.77 2.25007 6.5145767E+04 3.6728253E+07 563.79 2.26016 6.5051047E+04 3.6675851E+07 563.80 2.27009 6.4966735E+04 3.6629350E+07 563.82 2.28000 6.4871310E+04 3.6576445E+07 563.83 2.29019 6.4761651E+04 3.6515617E+07 563.85 2.30004 6.4647948E+04 3.6452469E+07 563.86 2.31012 6.4535167E+04 3.6389939E+07 563.88 2.32009 6.4424230E+04 3.6348461E+07 563.89 2.33002 6.4315209E+04 3.6268106E+07 563.91 2.34022 6.4206194E+04 3.6207774E+07 563.93 2.35007 6.4100408E+04 3.6149250E+07 563.95 2.36008 6.3989278E+04 3.6087769E+07 563.97 2.37011 6.3868104E+04 3.6020573E+07 563.98 2.38011 6.3745218E+04 3.5952544E+07 564.00 2.39013 6.3629468E+04 3.5888539E+07 564.02 2.40008 6.3516321E+04 3.5826065E+07 564.05 2.41016 6.3407662E+04 3.5766110E+07 564.07 2.42012 6.3298226E+04 3.5705745E+07 564.09 2.43004 6.3189783E+04 3.5645942E+07 564.11 2.44010 6.3079669E+04 3.5585210E+07 564.13 2.45013 6.2968324E+04 3.5523846E+07 564.15 2.46012 6.2858904E+04 3.5463541E+07 564.18 2.47009 7.2751233E+04 3.5414285E+07 564.20 2.48011 7.2649538E+04 3.5348400E+07 564.22 2.49010 7.2546417E+04 3.5291722E+07 564.25 2.50017 7.2441011E+04 3.5233761E+07 564.27 6.2.1-98 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 9 of 10) 2.51015 6.2360248E+04 3.5189781E+07 564.30 2.52017 6.2285701E+04 3.5149251E+07 564.32 2.53002 6.2213377E+04 3.5109968E+07 564.35 2.54011 6.2144447E+04 3.5072628E+07 564.37 2.55004 6.2074492E+04 3.5034700E+07 564.40 2.56011 6.2002522E+04 3.4995675E+07 564.42 2.57012 6.1925868E+04 3.4954001E+07 564.45 2.58007 6.1839278E+04 3.4906740E+07 564.48 2.59017 6.1751078E+14 3.4858631E+07 564.50 2.60012 6.1655475E+04 3.4806378E+07 564.53 2.61012 6.1557127E+04 3.4752559E+07 564.56 2.62017 6.1453393E+04 3.4695764E+07 564.59 2.63012 6.1345872E+04 3.4636880E+07 564.62 2.64017 6.1236417E+04 3.4576903E+07 564.65 2.65000 6.1120804E+04 3.4513455E+07 564.68 2.69015 6.0636936E+04 3.4247943E+07 564.80 2.70015 6.0514075E+04 3.4180534E+07 564.84 2.71015 6.0392973E+04 3.4114134E+07 564.87 2.72001 6.0275870E+04 3.4049934E+07 564.90 2.73007 6.0158531E+04 3.3985641E+07 564.93 2.74011 6.0146178E+04 3.3924017E+07 564.97 2.75004 5.9935107E+04 3.3863317E+07 565.00 2.76011 5.9827207E+04 3.3804290E+07 565.03 2.77002 5.9721999E+04 3.3746760E+07 565.06 2.78011 5.9617017E+04 3.3689833E+07 565.10 2.78012 5.9516318E+04 3.3634378E+07 565.13 2.80007 5.9424684E+04 3.3584464E+07 565.16 2.81011 5.9332760E+04 3.3534409E+07 565.19 2.82007 5.9239848E+04 3.3483771E+07 565.22 2.83021 5.9146625E+04 3.3432986E+07 565.26 2.84003 5.9056308E+04 3.3383826E+07 565.29 2.85010 5.8965263E+04 3.3334296E+07 565.32 2.86006 5.8878112E+04 3.3286969E+07 565.35 2.87012 5.8792590E+04 3.3240574E+07 565.39 2.88011 5.8703158E+04 3.3191991E+07 565.42 2.89003 5.8611039E+04 3.3141918E+07 565.46 2.90000 5.8516521E+04 3.3090534E+07 565.49 2.91008 5.8420275E+04 3.3038213E+07 565.53 2.92007 5.8323527E+04 3.2985689E+07 565.56 2.93019 5.8224442E+04 3.2931900E+07 565.60 2.94006 5.8124578E+04 3.2877642E+07 565.64 2.95006 5.8018131E+04 3.2819800E+07 565.68 2.96010 5.7908517E+04 3.2760201E+07 565.72 Containment Functional Design 6.2.1-99 | |||
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 10 of 10) 2.97010 5.7797561E+04 3.2699923E+07 565.77 2.98015 5.7687325E+04 3.2640079E+07 565.81 2.99002 5.7576594E+04 3.2580065E+07 565.86 3.00006 5.7464688E+04 3.2519421E+07 565.90 6.2.1-100 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-24 Break Mass And Energy Flow From A Double-Ended Hot Leg Guillotine Break (Page 1 of 7) | |||
Time Mass Flow Energy Flow Avg. Enthalpy (sec) (lbm/sec) (Btu/sec) (Btu/lbm) 0.00000 9.5000000E+03 6.1732900E+06 649.82 0.00250 8.3366021E+04 5.3981726E+07 647.53 0.00502 7.7261661E+04 4.9885082E+07 645.66 0.00751 6.9212037E+04 4.4671873E+07 645.44 0.01002 6.9198929E+04 4.4701697E+07 645.99 0.01251 7.0256102E+04 4.5378071E+07 645.90 0.01502 7.0488357E+04 4.5540990E+07 646.08 0.01750 7.1061056E+04 4.5928796E+07 646.33 0.02001 7.1751507E+04 4.6383734E+07 646.45 0.02251 7.2329964E+04 4.6764991E+07 646.55 0.02501 7.2847529E+04 4.7105934E+07 646.64 0.02751 7.3317785E+04 4.7415620E+07 646.71 0.03000 7.3729839E+04 4.7687553E+07 646.79 0.03251 7.4102693E+04 4.7933725E+07 646.86 0.03503 7.4425566E+04 4.8146411E+07 646.91 0.03750 7.4680137E+04 4.8313842E+07 646.94 0.04002 7.4861813E+04 4.8433649E+07 646.97 0.04251 7.4970099E+04 4.8506310E+07 647.01 0.04502 7.5032184E+04 4.8550423E+07 647.07 0.04750 7.5091651E+04 4.8596843E+07 647.17 0.05002 7.5182404E+04 4.8666717E+07 647.32 0.05252 7.5339506E+04 4.8784748E+07 647.53 0.05501 7.5615681E+04 4.8985032E+07 647.82 0.05752 7.6070086E+04 4.9303128E+07 648.13 0.06003 7.6618468E+04 4.9677350E+07 648.37 0.06250 7.7167510E+04 5.0046721E+07 648.55 0.06502 7.7719314E+04 5.0413314E+07 648.66 0.06751 7.8269593E+04 5.0773994E+07 648.71 0.07002 7.8788572E+04 5.1111466E+07 648.72 0.07255 7.9317101E+04 5.1952175E+07 648.69 0.07501 7.9810365E+04 5.1767914E+07 648.64 0.07753 8.0303796E+04 5.2081424E+07 648.55 0.08001 8.0766439E+04 5.2373661E+07 648.46 0.08252 8.1217125E+04 5.2656350E+07 648.34 0.08506 8.1642762E+04 5.2921379E+07 648.21 0.08756 8.2029389E+04 5.3160708E+07 648.07 0.09002 8.2387885E+04 5.3380563E+07 647.92 0.09250 8.2708495E+04 5.3574748E+07 647.75 0.09501 8.2989585E+04 5.3742451E+07 647.58 0.09753 8.3215688E+04 5.3873165E+07 647.39 0.10008 8.3360910E+04 5.3950565E+07 647.19 0.10251 8.3384152E+04 5.3948819E+07 646.99 Containment Functional Design 6.2.1-101 | |||
WATTS BAR WBNP-112 Table 6.2.1-24 Break Mass And Energy Flow From A Double-Ended Hot Leg Guillotine Break (Page 2 of 7) 0.10504 8.3224047E+04 5.3827401E+07 646.78 0.10758 8.2846812E+04 5.3565471E+07 646.56 0.11010 8.2310335E+04 5.3203143E+07 646.37 0.11251 8.1735809E+04 5.2818443E+07 646.21 0.11505 8.1098574E+04 5.2396220E+07 646.08 0.11757 8.0492200E+04 5.1995488E+07 645.97 0.12002 7.9906381E+04 5.1608231E+07 645.86 0.12255 7.9318382E+04 5.1220985E+07 645.76 0.12510 7.8761980E+04 5.0855277E+07 645.68 0.12764 7.8253342E+04 5.0521446E+07 645.61 0.13016 7.7799330E+04 5.0223807E+07 645.56 0.13263 7.7397664E+04 4.9959595E+07 645.49 0.13508 7.7031158E+04 4.9718321E+07 645.43 0.13762 7.6689163E+04 4.9492689E+07 645.37 0.14012 7.6380797E+04 4.9287963E+07 645.29 0.14260 7.6093060E+04 4.9096220E+07 645.21 0.14502 7.5829184E+04 4.8919745E+07 645.13 0.14758 7.5565368E+04 4.8742549E+07 645.04 0.15014 7.5315976E+04 4.8574325E+07 644.94 0.15256 7.5093228E+04 4.8423506E+07 644.83 0.15502 7.4878984E+04 4.8277964E+07 644.75 0.15758 7.4673649E+04 4.8137969E+07 644.64 0.16009 7.4492138E+04 4.8013597E+07 644.55 0.16260 7.4333611E+04 4.7904109E+07 644.45 0.16519 7.4195208E+04 4.7807226E+07 644.34 0.16754 7.4087107E+04 4.7730165E+07 644.24 0.17019 7.3982177E+04 4.7654413E+07 644.13 0.17254 7.3903197E+04 4.7595794E+07 644.03 0.17519 7.3821471E+04 4.7533480E+07 643.90 0.17758 7.3750923E+04 4.7478555E+07 643.77 0.18002 7.3679828E+04 4.7422428E+07 643.63 0.18270 8.3600631E+04 4.7359686E+07 643.47 0.18511 8.3530498E+04 4.7303918E+07 643.32 0.18772 8.3456456E+04 4.7244677E+07 643.17 0.19014 8.3391431E+04 4.7192111E+07 643.02 0.19261 8.3329933E+04 4.7141607E+07 642.87 0.19518 8.3272436E+04 4.7041292E+07 642.71 0.19762 8.3221499E+04 4.7049902E+07 642.57 0.20002 8.3178925E+04 4.7012004E+07 642.43 0.20252 8.3137257E+04 4.6974010E+07 642.27 0.20503 8.3098113E+04 4.6937497E+07 642.12 0.20750 8.3060530E+04 4.6902038E+07 641.96 6.2.1-102 Containment Functional Design | |||
===2.0 | WATTS BAR WBNP-112 Table 6.2.1-24 Break Mass And Energy Flow From A Double-Ended Hot Leg Guillotine Break (Page 3 of 7) 0.21008 7.3019492E+04 4.6863606E+07 641.80 0.21271 7.2971863E+04 4.6820468E+07 641.62 0.21504 7.2924285E+04 4.6778800E+07 641.47 0.21762 7.2863276E+04 4.6727166E+07 641.30 0.22021 7.2792031E+04 4.6668884E+07 641.13 0.22253 7.2719274E+04 4.6611036E+07 640.97 0.22502 7.2632208E+04 4.6543311E+07 640.81 0.22772 7.2528486E+04 4.6469108E+07 640.63 0.23020 7.2 24247E+04 4.6385682E+07 640.47 0.23265 7.2315195E+04 4.6304601E+07 640.32 0.23510 7.2201162E+04 4.6220523E+07 640.16 0.23754 7.2042610E+04 4.6133707E+07 640.01 0.24018 7.1951100E+04 4.6037989E+07 639.85 0.24256 7.1830885E+04 4.5950825E+07 639.71 0.24520 7.1697100E+04 4.5853958E+07 639.55 0.24769 7.1572088E+04 4.5763462E+07 639.40 0.25022 7.1446885E+04 4.5672780E+07 639.26 0.25255 7.1334337E+04 4.5591101E+07 639.12 0.25518 7.1211486E+04 4.5501645E+07 638.96 0.25761 7.1102069E+04 4.5421652E+07 638.82 0.26008 7.0995474E+04 4.5343313E+07 638.68 0.26261 7.0891562E+04 4.5266449E+07 638.53 0.26519 7.0790622E+04 4.5191236E+07 638.38 0.26733 7.0702525E+04 4.5125078E+07 638.24 0.27009 7.0611282E+04 4.5056173E+07 638.09 0.27266 7.0523851E+04 4.4989715E+07 637.94 0.27520 7.0442164E+04 4.4926984E+07 637.79 0.27758 7.0368655E+04 4.4869978E+07 637.64 0.28017 7.0292576E+04 4.4810367E+07 637.48 0.28254 7.0224050E+04 4.4756397E+07 637.34 0.28513 7.0151601E+04 4.4699085E+07 637.18 0.28770 7.0081456E+04 4.4643369E+07 637.02 0.29012 7.0015740E+04 4.4591188E+07 636.87 0.29270 6.9947068E+04 4.4536538E+07 636.72 0.29504 6.9885463E+04 4.4487471E+07 636.58 0.29760 6.9818055E+04 4.4433794E+07 636.42 0.30018 6.9750621E+04 4.4380130E+07 636.27 0.302 5 6.9688876E+04 4.4331051E+07 636.13 0.30520 6.9619964E+04 4.4276364E+07 635.97 0.30766 6.9555942E+04 4.4225658E+07 635.83 0.31020 6.9490098E+04 4.4173606E+07 635.68 0.31256 6.9428756E+04 4.4125198E+07 635.55 Containment Functional Design 6.2.1-103 | ||
: 4. | WATTS BAR WBNP-112 Table 6.2.1-24 Break Mass And Energy Flow From A Double-Ended Hot Leg Guillotine Break (Page 4 of 7) 0.31502 6.9364785E.04 4.4074786E+07 635.41 0.31776 6.9292945E+04 4.4018417E+07 635.25 0.32026 6.9228329E+04 4.3967794E+07 635.11 0.32278 6.9162511E+04 4.3916352E+07 634.97 0.32500 6.9104546E+04 4.3871173E+07 634.85 0.32751 6.9039481E+04 4.3820519E+07 634.72 0.33003 6.8974226E+04 4.3769791E+07 634.58 0.33255 6.8909148E+04 4.3719287E+07 634.45 0.33507 6.8844266E+04 4.3669001E+07 634.32 0.33759 6.8779396E+04 4.3618794E+07 634.18 0.34012 6.8714551E+04 4.3568709E+07 634.05 0.34264 6.8679846E+04 4.3518771E+07 633.42 0.34517 6.8585131E+04 4.3468932E+07 633.80 0.34770 6.8520434E+04 4.3418197E+07 633.67 0.35022 6.8455793E+04 4.3369591E+07 633.54 0.35275 6.8391227E+04 4.3320125E+07 633.42 0.35528 6.8326749E+04 4.3270811E+07 633.29 0.35753 6.8269558E+04 4.3227127E+07 633.18 0.36006 6.8205347E+04 4.3179176E+07 633.06 0.36260 6.8141484E+04 4.3129458E+07 632.44 0.36514 6.8077896E+04 4.3081018E+07 632.82 0.34769 6.8014722E+04 4.3032888E+07 632.70 0.37076 6.7952063E+04 4.2985130E+07 632.58 0.37255 6.7896887E+04 4.2943032E+07 632.47 0.37515 6.7835502E+04 4.2896141E+07 632.36 0.37777 6.7775061E+04 4.2849802E+07 632.24 0.38012 6.7722086E+04 4.2809071E+07 632.13 0.38280 6.7663597E+04 4.2763911E+07 632.01 0.38521 6.7612661E+04 4.2724370E+07 631.90 0.38766 6.7562816E+04 4.2685441E+07 631.79 0.39014 6.7514175E+04 4.2647182E+07 631.68 0.39267 6.7466809E+04 4.2609616E+07 631.56 0.39525 6.7420771E+04 4.2572755E+07 631.45 0.39755 6.7381410E+04 4.2541088E+07 631.35 0.40024 6.7338142E+04 4.2505555E+07 631.23 0.40263 6.7301204E+04 4.2475007E+07 631.12 0.40505 6.7265696E+04 4.2445335E+07 631.01 0.40754 6.7230577E+04 4.2415619E+07 630.90 0.41008 6.7196212E+04 4.2368271E+07 630.78 0.41265 6.7162616E+04 4.2357391E+07 630.67 0.41522 6.7129564E+04 4.2328625E+07 630.55 0.41759 6.7099339E+04 4.2302439E+07 630.44 6.2.1-104 Containment Functional Design | ||
WATTS BAR WBNP-112 Table 6.2.1-24 Break Mass And Energy Flow From A Double-Ended Hot Leg Guillotine Break (Page 5 of 7) 0.42016 6.7047039E+04 4.2274388E+06 630.33 0.42263 6.7035782E+04 4.2247295E+07 630.22 0.42509 6.7004568E+04 4.2220317E+07 630.11 0.42767 6.6971284E+04 4.2191629E+07 630.00 0.43024 6.6936789E+04 4.2162210E+07 629.88 0.43281 6.6901398E+04 4.2132309E+07 629.77 0.43510 6.6868952E+04 4.2105162E+07 629.67 0.43779 6.6829329E+04 4.2072364E+07 629.55 0.44015 6.6792662E+04 4.204242 E+07 629.45 0.44263 6.6752389E+04 4.2010062E+07 629.34 0.44503 6.6712436E+04 4.1978278E+07 629.24 0.44776 6.6669435E+04 4.1941233E+07 629.13 0.45031 6.6620128E+04 4.1905799E+07 629.03 0.45260 6.6577783E+04 4.1872966E+07 628.93 0.45518 6.6529174E+04 4.1835621E+07 628.83 0.45779 6.6474055E+04 4.1797358E+07 628.73 0.46006 6.6434522E+04 4.1763609E+07 628.64 0.46262 6.6383646E+04 4.1725280E+07 628.55 0.46518 6.6332450E+04 4.1686877E+07 628.45 0.46775 6.6280967E+04 4.1648404E+07 628.36 0.47030 6.6229638E+04 4.1610156E+07 628.27 0.47255 6.6184 40E+04 4.1576904E+07 628.19 0.47512 6.6134141E+04 4.1539141E+07 628.10 0.47771 6.6083853E+04 4.1501763E+07 628.02 0.48032 6.6034259E+04 4.1464870E+07 627.93 0.18262 6.5991507E+04 4.1433014E+07 627.85 0.18527 6.5943495E+04 4.1397152E+07 627.77 0.18762 6.5902325E+04 4.1366304E+07 627.69 0.49034 6.5856311E+04 4.1331688E+07 627.60 0.49274 6.5817000E+04 4.1301975E+07 627.51 0.49517 6.5778874E+04 4.1273019E+07 627.45 0.49765 6.5741321E+04 4.1244325E+07 627.37 0.50024 6.5703604E+04 4.1215508E+07 627.29 0.51012 6.5570446E+04 4.1111667E+07 626.98 0.52016 6.5456120E+04 4.1020126E+07 626.68 0.53003 6.5347836E+04 4.0933067E+07 626.39 0.54020 6.5234080E+04 4.0842628E+07 626.09 0.55004 6.5114485E+04 4.0750005E+07 625.82 0.56004 6.4980058E+04 4.0644890E+07 625.56 0.57018 6.4832681E+04 4.0540699E+07 625.31 0.58018 6.4683520E+04 4.0432982E+07 625.09 0.59033 6.4537352E+04 4.0328174E+07 624.88 Containment Functional Design 6.2.1-105 | |||
WATTS BAR WBNP-112 Table 6.2.1-24 Break Mass And Energy Flow From A Double-Ended Hot Leg Guillotine Break (Page 6 of 7) 0.60028 6.4405682E+04 4.0233863E+07 624.69 0.61006 6.4291379E+04 4.0151570E+07 624.52 0.62028 6.4185296E+04 4.0074475E+07 624.36 0.63028 6.4088543E+04 4.0003799E+07 624.20 0.64037 6.3991051E+04 3.9932853E+07 624.04 0.65032 6.3890693E+04 3.9860535E+07 623.89 0.66003 6.3787662E+04 3.9787307E+07 623.75 0.67035 6.3673290E+04 3.970717 E+07 623.61 0.68020 6.3560494E+04 3.9629252E+07 623.49 0.69008 6.3444844E+04 3.9550368E+07 623.38 0.70037 6.3323594E+04 3.9468650E+07 623.29 0.71029 6.3206689E+04 3.9390687E+07 623.20 0.72021 6.3092848E+04 3.9315454E+07 623.14 0.73010 6.2978206E+04 3.9240792E+07 623.09 0.74021 6.2863312E+04 3.9166115E+07 623.04 0.75002 6.2754080E+04 3.9094680E+07 622.98 0.76000 6.2641845E+04 3.9021892E+07 622.94 0.77025 6.2527645E+04 3.8948268E+07 622.90 0.78006 6.2420690E+04 3.8879349E+07 622.86 0.79033 6.2310561E+04 3.8809018E+07 622.83 0.80016 6.2205817E+04 3.8742510E+07 622.81 0.81028 6.2097447E+04 3.8674058E+07 622.80 0.82032 6.1988143E+04 3.8605382E+07 622.79 0.83026 6.1877208E+04 3.8536023E+07 622.78 0.84010 6.1764525E+04 3.8465890E+07 622.78 0.85016 6.1646530E+04 3.8392779E+07 622.79 0.86014 6.1528079E+04 3.8319750E+07 622.80 0.87013 6.1410582E+04 3.8247723E+07 622.82 0.88014 6.1295125E+04 3.8177357E+07 622.84 0.89016 6.1181918E+04 3.8108690E+07 622.88 0.90014 6.1070276E+04 3.8041150E+07 622.91 0.91001 6.0959110E+04 3.7973934E+07 622.94 0.92006 6.0843976E+04 3.7904302E+07 622.98 0.93002 6.0728862E+04 3.7834735E+07 623.01 0.94022 6.0611678E+04 3.7764186E+07 623.05 0.95016 6.0502372E+04 3.7698968E+07 623.10 0.96032 6.0399882E+04 3.7638703E+07 623.16 0.97003 6.0310970E+04 3.7587283E+07 623.22 0.98019 6.0224576E+04 3.7537977E+07 623.30 0.99034 6.0141262E+04 3.7490808E+07 623.38 1.00009 6.0061803E+04 3.7446007E+07 623.46 1.05030 5.9639533E+04 3.7210078E+07 623.92 6.2.1-106 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-24 Break Mass And Energy Flow From A Double-Ended Hot Leg Guillotine Break (Page 7 of 7) 1.10009 5.9161129E+04 3.6942041E+07 624.43 1.15005 5.8600069E+04 3.6621801E+07 624.94 1.20022 5.8110574E+04 3.6350936E+07 625.55 1.25009 5.7618787E+04 3.6075665E+07 626.11 1.30021 5.7172718E+04 3.5828693E+07 626.67 1.35018 5.6709129E+04 3.5567732E+07 627.20 1.40030 5.6244826E+04 3.5305636E+07 627.71 1.45011 5.5752608E+04 3.5023683E+07 628.20 1.50013 5.5230766E+04 3.4722152E+07 628.67 1.55010 5.4683919E+04 3.4403984E+07 629.14 1.60014 5.4098362E+04 3.4059730E+07 629.59 1.65001 5.3515705E+04 3.3718514E+07 630.07 1.70007 5.2934335E+04 3.3379803E+07 630.59 1.75010 5.2337170E+04 3.3032036E+07 631.14 1.80003 5.1749965E+04 3.2692856E+07 631.75 1.85003 5.1168201E+04 3.2359058E+07 632.41 1.90028 5.0574787E+04 3.2018724E+07 633.10 1.95028 4.9983327E+04 3.1680180E+07 633.81 2.00032 4.9412836E+04 3.1356166E+07 634.58 Containment Functional Design 6.2.1-107 | |||
WATTS BAR WBNP-112 Table 6.2.1-25 Double-Ended Pump Suction LOCA Sequence of Events Event Time (sec) | |||
Rupture 0.0 Accumulator Flow Starts 15.6 Assumed Initiation of ECCS 36.13 End of Blowdown 26.8 Accumulators Empty 66.700 Assumed Initiation of Spray System 234.0 End of Reflood 239.8 Low Level Alarm of Refueling Water Storage Tank 1,207.27 Beginning of Recirculation Phase of Safeguards Operation 1,267.27 6.2.1-108 Containment Functional Design | |||
Containment Functional Design WATTS BAR Table 6.2.1-26a Double-Ended Pump Suction Guillotine Break Minimum Safety Injection - Mass Balance Start of End of Bottom of End of Broken Loop Intact Loop SG Mass Balance Accident Blowdown Core Reflood SG Equilibration Recovery Equilibration Time 0.00 26.80 26.80 239.78 910.84 2267.21 (Seconds) | |||
Mass (Thousands lbm) | |||
Initial In RCS and 750.32 750.32 750.32 750.32 750.32 750.32 ACC Added Mass Pumped 0.00 0.00 0.00 124.49 552.04 1220.31 Injection Total 0.00 0.00 0.00 124.49 552.04 1220.31 Added | |||
***Total Available*** 750.32 750.32 750.32 874.81 1302.36 1970.63 Distribution Reactor 492.76 73.81 73.95 135.56 135.56 135.56 Coolant Accumulato 257.56 178.44 178.31 0.00 0.00 0.00 r | |||
Total 750.32 252.25 252.25 135.56 135.56 135.56 Contents Effluent Break Flow 0.00 498.05 498.05 728.64 1156.19 18.24.25 ECCS Spill 0.00 0.00 0.00 0.00 0.00 .00 Total 0.00 498.05 498.05 728.64 1156.19 1824.25 Effluent WBNP-112 | |||
***Total Accountable*** 750.32 750.30 750.30 864.20 1291.76 1959.81 6.2.1-109 | |||
6.2.1-110 WATTS BAR Table 6.2.1-26b Double-Ended Pump Suction Guillotine Break Minimum Safety Injection - Energy Balance Start of End of Bottom of End of Broken Loop Intact Loop Mass Balance Accident Blowdown Core Reflood SG SG Recovery Equilibration Equilibration Time (Seconds) 0.00 26.80 26.80 239.78 910.84 2267.21 Energy (Million Btu) | |||
Initial Energy In RCS, ACC, S Gen 897.41 897.41 897.41 897.41 897.41 897.41 Added Energy Pumped Injection 0.00 0.00 0.00 9.10 40.33 99.28 Decay Heat 0.00 7.71 7.71 31.38 86.67 172.38 Heat from Secondary 0.00 12.38 12.38 12.38 19.63 31.54 Total Added 0.00 20.08 20.08 52.85 146.62 303.20 | |||
***Total Available*** 897.41 917.50 917.50 950.26 1044.04 1200.61 Distribution Reactor Coolant 296.93 13.38 13.39 30.09 30.09 30.09 Accumulator 25.62 17.75 17.73 0.00 0.00 0.00 Core Stored 25.61 14.17 14.17 3.98 3.62 3.47 Primary Metal 159.12 151.04 151.04 134.36 82.72 58.16 Containment Functional Design Secondary Metal 104.98 104.40 104.40 95.12 70.79 43.31 Steam Generator 285.15 301.24 301.24 269.84 201.52 132.64 Total Contents 897.41 601.98 601.98 533.39 388.74 267.68 WBNP-112 | |||
WATTS BAR WBNP-112 Table 6.2.1-27a Steam Line Break Blowdown Mass Flow Rate, m Energy Flow Rate, e Time (sec) (lbm/sec) (106 Btu/sec) 0 14214 16.898 1.34 14214 16.898 1.94 15260 17.267 2.25 16577 17.975 2.26 36873 23.556 2.84 39326 24.118 3.84 40907 24.621 5.34 41441 24.779 10.34 41111 24.682 13.34 40195 24.400 17.34 38536 23.858 Containment Functional Design 6.2.1-111 | |||
WATTS BAR WBNP-112 Table 6.2.1-27b Steam Generator Enclosure Geometry Nodes Volume (ft3) 51, 56 5551 52, 57 1688 53, 58 1695 54, 59 1826 55, 60 1836 6.2.1-112 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-27c Steam Generator Enclosure Flow Path Data LI DH A LEQ Path k F (ft) (ft) (ft²) (ft) a/A H51 1.50 0.02 13.30 8.70 170.90 4.00 0.58 H52, H57 0.86 0.02 5.20 4.50 33.20 1.20 0.23 H53, H58 0.96 0.02 4.10 3.20 23.90 0.30 0.17 H54, H59 0.86 0.02 5.20 5.60 41.80 1.20 0.28 H55, H60 0.96 0.02 4.10 5.80 43.80 0.30 0.32 R51, R56 0.24 0.02 9.40 6.40 114.00 7.60 0.27 R52, R57 0.00 0.02 14.80 6.40 114.00 14.80 1.00 R53, R58 0.00 0.02 14.80 7.70 115.00 14.80 1.00 R54, R59 1.50 0.02 5.00 5.30 87.00 3.00 0.70 R55, R60 1.50 0.02 5.50 6.30 93.90 3.40 0.75 A51, A56 0.23 0.02 9.40 7.70 115.00 7.60 0.27 Containment Functional Design 6.2.1-113 | |||
WATTS BAR WBNP-112 Table 6.2.1-27d Peak Differential Pressure - Steam Generator Enclosure Across Enclosure Walls Nodes Differential Pressure (psi) Time (sec) 51 - Upper Compartment 28.8 5.52 52 - Upper Compartment 27.9 5.54 53 -Upper Compartment 27.9 5.54 54 - Upper Compartment 27.7 5.56 55 -Upper Compartment 27.7 5.56 Across Steam Generator Vessel Nodes Differential Pressure (psi) Time (sec) 53-52 0.03 0.017 55-54 0.08 0.039 Across Steam Generator Separator Wall Nodes Differential Press. (psi) Time (sec) 55-59 11.00 0.040 6.2.1-114 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-28 Mass And Energy Release Rates Into Pressurizer Enclosure Time (sec) Mass Flow (103 lbm/sec) Energy Flow (106 Btu/sec) 0.0 0.0 0.0 0.00251 5.0473 3.0977 0.00502 5.2333 3.2013 0.01002 5.1051 3.1226 0.01251 5.0746 3.1029 0.01755 5.3833 3.2753 0.02505 5.5402 3.3601 0.03259 5.8746 3.5479 0.04002 5.9221 3.5716 0.05005 5.6865 3.4332 0.07250 5.7877 3.4868 0.09001 5.4917 3.3157 0.11253 5.9404 3.5710 0.13756 5.5454 3.3445 0.15755 5.6392 3.3979 0.17760 5.4721 3.3026 0.19254 5.5189 3.3291 0.21254 5.4725 3.3025 0.23508 5.5465 3.3446 0.27752 5.5345 3.3378 0.35027 5.3649 3.2411 0.38001 5.2985 3.2031 0.41515 5.3825 3.2507 0.45006 5.2660 3.1842 0.57002 5.2492 3.1738 0.77015 5.1816 3.1336 1.00005 5.1562 3.1169 2.00015 5.0326 3.0400 Containment Functional Design 6.2.1-115 | |||
WATTS BAR WBNP-112 Table 6.2.1-29a Pressurizer Geometric Data Node Volume (ft3) 51 2262 52 502 53 667 54 647 Flow Path k f L1(ft) DH(ft) A(ft2) LEQ(ft) a/A 51-52 0.5 0.02 13.3 3.3 20.9 12.1 0.16 51-53 0.5 0.02 13.8 4.8 27.7 12.1 0.21 51-54 0.5 0.02 13.8 4.8 26.9 12.1 0.21 53-52 0.0 0.02 8.0 3.5 42.6 8.0 0.28 54-52 0.0 0.02 8.0 1.5 18.5 8.0 0.12 53-54 0.0 0.02 8.0 0.9 11.3 8.0 0.06 52-lower 1.0 0.02 12.0 3.3 22.1 12.0 1.00 compartment 53-lower 1.0 0.02 12.0 4.8 27.7 12.0 1.00 compartment 54-lower 1.0 0.02 12.0 4.8 24.4 12.0 1.00 compartment 6.2.1-116 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-29b Peak Differential Pressure - Pressurizer Enclosure Across Enclosure Walls Nodes Differential Press. (psi) Time (sec) 51 - Upper Compartment 11.4 0.06 52 - Upper Compartment 7.7 0.10 53 - Upper Compartment 7.7 0.10 54 - Upper Compartment 7.7 0.10 Across Pressurizer Vessel Nodes Differential Press. (psi) Time (sec) 52 - 53 -0.04 0.038 52 - 54 -0.23 0.046 53 - 54 -0.20 0.050 Containment Functional Design 6.2.1-117 | |||
WATTS BAR WBNP-112 Table 6.2.1-30 Mass And Energy Release Rates 127 in2 Cold Leg (Page 1 of 5) | |||
Time Mass Flow Energy Flow Avg. Enthalpy (sec) (lbm/sec) (Btu/sec) (Btu/lbm) 0.00000 0. 0. 0.00 0.00251 1.1982845E+04 6.7296740E+06 561.61 0.00502 1.5308269E+04 8.5974676E+06 561.62 0.00751 1.7398501E+04 9.7720743E+06 561.66 0.01001 1.9131092E+04 1.0741761E+07 561.48 0.01253 1.9948352E+04 1.1193906E+07 561.14 0.01503 1.9716482E+04 1.1050978E+07 560.49 0.01753 2.1905036E+04 1.2288321E+07 560.98 0.02006 2.2170478E+04 1.2426731E+07 560.51 0.02255 2.1560830E+04 1.2069870E+07 559.81 0.02506 2.1315153E+04 1.1923450E+07 559.39 0.02751 2.1626356E+04 1.2094688E+07 559.26 0.03001 2.1729350E+04 1.2147779E+07 559.05 0.03254 2.2084361E+04 1.2345775E+07 559.03 0.03503 2.2542872E+04 1.2603165E+07 559.08 0.03757 2.2895385E+04 1.2800602E+07 559.09 0.04009 2.3203939E+04 1.2973383E+07 559.10 0.04255 2.3446963E+04 1.3108981E+07 559.09 0.04502 2.3464854E+04 1.3115753E+07 558.95 0.04752 2.3298089E+04 1.3017402E+07 558.73 0.05001 2.3145127E+04 1.2927663E+07 558.55 0.05266 2.3018004E+04 1.2853122E+07 558.39 0.05514 2.2950194E+04 1.2812973E+07 558.29 0.05757 2.2904460E+04 1.2785675E+07 558.22 0.06012 2.2779154E+04 1.2713027E+07 558.10 0.06257 2.2510846E+04 1.2559119E+07 557.91 0.06500 2.2164087E+04 1.2360966E+07 557.70 0.06763 2.1888594E+04 1.2203861E+07 557.54 0.07009 2.1850009E+04 1.2182079E+07 557.53 0.07259 2.2019590E+04 1.2278820E+07 557.63 0.07503 2.2242956E+04 1.2406073E+07 557.75 0.07759 2.2352310E+04 1.2468054E+07 557.80 0.08002 2.2278656E+04 1.2425609E+07 557.74 0.08253 2.2036897E+04 1.2287536E+07 557.59 0.08504 2.1670113E+04 1.2078517E+07 557.38 0.08752 2.1266578E+04 1.1848983E+07 557.16 0.09004 2.0857542E+04 1.1617001E+07 556.97 0.09260 2.0466616E+04 1.1395523E+07 556.79 0.09500 2.0201194E+04 1.1245397E+07 556.67 0.09751 2.0053059E+04 1.1161858E+07 556.62 0.10007 2.0025022E+04 1.1146521E+07 556.63 6.2.1-118 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-30 Mass And Energy Release Rates 127 in2 Cold Leg (Page 2 of 5) | |||
Time Mass Flow Energy Flow Avg. Enthalpy (sec) (lbm/sec) (Btu/sec) (Btu/lbm) 0.10515 2.0170943E+04 1.1230305E+07 556.76 0.11011 2.0365487E+04 1.1341279E+07 556.89 0.11505 2.0647554E+04 1.1501747E+07 557.05 0.12008 2.0944972E+04 1.1670752E+07 557.21 0.12502 2.0977664E+04 1.1688856E+07 557.20 0.13007 2.0780412E+04 1.1576250E+07 557.08 0.13509 2.0500682E+04 1.1417226E+07 557.92 0.14001 2.0096382E+04 1.1187990E+07 556.72 0.14508 1.9569603E+04 1.0889944E+07 556.47 0.15009 1.9235427E+04 1.0701397E+07 556.34 0.15504 1.9138491E+04 1.0647134E+07 556.32 0.16006 1.9034644E+04 1.0588880E+07 556.30 0.16505 1.8879080E+04 1.0501358E+07 556.24 0.17007 1.8748148E+04 1.0427857E+07 556.21 0.17514 1.8720580E+04 1.0412805E+07 556.22 0.18005 1.8785810E+04 1.0450146E+07 556.28 0.18504 1.8911550E+04 1.0521664E+07 556.36 0.19010 1.9101126E+04 1.0629209E+07 556.47 0.19507 1.9311878E+04 1.0748514E+07 556.58 0.20009 1.9465602E+04 1.0835436E+07 556.65 0.21252 1.9617023E+04 1.0920644E+07 556.69 0.22507 1.9458748E+04 1.0830336E+07 556.58 0.23759 1.9647389E+04 1.0937376E+07 556.68 0.25011 1.9804565E+04 1.1026138E+07 556.75 0.26253 1.9395307E+04 1.0793667E+07 556.51 0.27516 1.8760813E+04 1.0435112E+07 556.22 0.28761 1.8860759E+04 1.0492777E+07 556.33 0.30014 1.9381793E+04 1.0787950E+07 556.60 0.31261 1.9557340E+04 1.0886714E+07 556.66 0.32509 1.9428795E+04 1.0813221E+07 556.56 0.33757 1.9460687E+04 1.0831309E+07 556.57 0.35003 1.9510288E+04 1.0859152E+07 556.59 0.36251 1.9334731E+04 1.0759415E+07 556.48 0.37512 1.9237392E+04 1.0704384E+07 556.44 0.38764 1.9172556E+04 1.0667882E+07 556.41 0.40007 1.9255351E+04 1.0715044E+07 556.47 0.41263 1.9518505E+04 1.0864131E+07 556.61 0.42512 1.9566788E+04 1.0890843E+07 556.60 0.43769 1.9443279E+04 1.0820460E+07 556.51 0.45005 1.9309158E+04 1.0744438E+07 556.44 0.46260 1.9325193E+04 1.0753755E+07 556.46 Containment Functional Design 6.2.1-119 | |||
WATTS BAR WBNP-112 Table 6.2.1-30 Mass And Energy Release Rates 127 in2 Cold Leg (Page 3 of 5) | |||
Time Mass Flow Energy Flow Avg. Enthalpy (sec) (lbm/sec) (Btu/sec) (Btu/lbm) 0.47515 1.9427001E+04 1.0811564E+07 556.52 0.48751 1.9463982E+04 1.0832327E+07 556.53 0.50010 1.9412566E+04 1.0802979E+07 556.49 0.52505 1.9416927E+04 1.0805655E+07 556.51 0.55001 1.9520981E+04 1.0864335E+07 556.55 0.57500 1.9439249E+04 1.0817886E+07 556.50 0.60009 1.9432289E+04 1.0814194E+07 556.51 0.62502 1.9570908E+04 1.0892620E+07 556.57 0.65001 1.9484134E+04 1.0843384E+07 556.52 0.67502 1.9537413E+04 1.0873742E+07 556.56 0.70006 1.9557525E+04 1.0885106E+07 556.57 0.72503 1.9556471E+04 1.0884559E+07 556.57 0.75008 1.9566953E+04 1.0890551E+07 556.58 0.77503 1.9575425E+04 1.0895394E+07 556.59 0.80011 1.9613175E+04 1.0916838E+07 556.61 0.82503 1.9623035E+04 1.0922366E+07 556.61 0.85012 1.9607042E+04 1.0913377E+07 556.60 0.87505 1.9625149E+04 1.0923689E+07 556.62 0.90005 1.9642366E+04 1.0933451E+07 556.63 0.92504 1.9652418E+04 1.0939158E+07 556.63 0.95005 1.9665495E+04 1.0946566E+07 556.64 0.97509 1.9657157E+04 1.0941870E+07 556.64 1.00024 1.9674801E+04 1.0951903E+07 556.65 1.02501 1.9674211E+04 1.0951587E+07 556.65 1.05002 1.9685832E+04 1.0958208E+07 556.65 1.07501 1.9689581E+04 1.0960360E+07 556.66 1.10003 1.9688612E+04 1.0959861E+07 556.66 1.12501 1.9688440E+04 1.0959833E+07 556.66 1.15013 1.9691682E+04 1.0961746E+07 556.67 1.17512 1.9694412E+04 1.0963374E+07 556.67 1.20008 1.9690643E+04 1.0961334E+07 556.68 1.22506 1.9686074E+04 1.0958870E+07 556.68 1.25010 1.9682378E+04 1.0956913E+07 556.69 1.27506 1.9685597E+04 1.0958900E+07 556.70 1.30002 1.9688096E+04 1.0960455E+07 556.70 1.32505 1.9673388E+04 1.0952302E+07 556.71 1.35006 1.9668391E+04 1.0949690E+07 556.72 1.37504 1.9669445E+04 1.0950509E+07 556.73 1.40009 1.9673705E+04 1.0950139E+07 556.74 1.42508 1.9668652E+04 1.0950505E+07 556.75 1.45004 1.9667081E+04 1.0950053E+07 556.76 6.2.1-120 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-30 Mass And Energy Release Rates 127 in2 Cold Leg (Page 4 of 5) | |||
Time Mass Flow Energy Flow Avg. Enthalpy (sec) (lbm/sec) (Btu/sec) (Btu/lbm) 1.47501 1.9675943E+04 1.0955165E+07 556.78 1.50004 1.9668050E+04 1.0950970E+07 556.79 1.52500 1.9665596E+04 1.0949895E+07 556.80 1.55005 1.9671043E+04 1.0953307E+07 556.82 1.57502 1.9666568E+04 1.0951104E+07 556.84 1.60008 1.9662702E+04 1.0949279E+07 556.86 1.62509 1.9658419E+04 1.0947234E+07 556.87 1.65008 1.9652327E+04 1.0944186E+07 556.89 1.67508 1.9641445E+04 1.0938449E+07 556.91 1.70000 1.9631684E+04 1.0933366E+07 556.92 1.72523 1.9622211E+04 1.0928465E+07 556.94 1.75002 1.9611372E+04 1.0922805E+07 556.96 1.77506 1.9600265E+04 1.0917009E+07 556.98 1.80004 1.9586316E+04 1.0909616E+07 556.00 1.82507 1.9570844E+04 1.0901377E+07 557.02 1.85004 1.9558044E+04 1.0894662E+07 557.04 1.87501 1.9547428E+04 1.0889183E+07 557.06 1.90005 1.9533703E+04 1.0881955E+07 557.09 1.92505 1.9518588E+04 1.0873945E+07 557.11 1.95013 1.9504270E+04 1.0866400E+07 557.13 1.97508 1.9490671E+04 1.0854264E+07 557.15 2.00001 1.9475975E+04 1.0851512E+07 557.17 2.02504 1.9460138E+04 1.0843124E+07 557.20 2.05011 1.9443525E+04 1.0834315E+07 557.22 2.07503 1.9425610E+04 1.0824775E+07 557.24 2.10004 1.9406458E+04 1.0814547E+07 557.27 2.12507 1.9386749E+04 1.0804030E+07 557.29 2.15003 1.9366596E+04 1.0793269E+07 557.31 2.17504 1.9344857E+04 1.0781622E+07 557.34 2.20000 1.9321966E+04 1.0769339E+07 557.36 2.22510 1.9298174E+04 1.0756568E+07 557.39 2.25001 1.9274722E+04 1.0743996E+07 557.41 2.27507 1.9250836E+04 1.0731182E+07 557.44 2.30008 1.9225729E+04 1.0717684E+07 557.47 2.32510 1.9199767E+04 1.0703706E+07 557.49 2.35000 1.9189974E+04 1.0698897E+07 557.53 2.37503 1.9159580E+04 1.0682347E+07 557.55 2.40011 1.9117138E+04 1.0659079E+07 557.57 2.42510 1.9108543E+04 1.0654963E+07 557.60 2.45013 1.9096201E+04 1.0648650E+07 557.63 2.47510 1.9042948E+04 1.0633130E+07 557.65 Containment Functional Design 6.2.1-121 | |||
WATTS BAR WBNP-112 Table 6.2.1-30 Mass And Energy Release Rates 127 in2 Cold Leg (Page 5 of 5) | |||
Time Mass Flow Energy Flow Avg. Enthalpy (sec) (lbm/sec) (Btu/sec) (Btu/lbm) 2.50011 1.9042948E+04 1.0619918E+07 557.68 2.52510 1.9038224E+04 1.0617984E+07 557.72 2.55010 1.9011234E+04 1.0603416E+07 557.74 2.57508 1.8977430E+04 1.0585017E+07 557.77 2.60006 1.8963744E+04 1.0578049E+07 557.80 2.62512 1.8950653E+04 1.0571411E+07 557.84 2.65025 1.8927642E+04 1.0559161E+07 557.87 2.67504 1.8894421E+04 1.0541167E+07 557.90 2.70018 1.8869044E+04 1.0527674E+07 557.93 2.72514 1.8846108E+04 1.0515517E+07 557.97 2.75003 1.8827068E+04 1.0505586E+07 558.00 2.77504 1.8815133E+04 1.0499666E+07 558.04 2.80005 1.8795707E+04 1.0489482E+07 558.08 2.82511 1.8768598E+04 1.0474967E+07 558.11 2.85006 1.8741259E+04 1.0460340E+07 558.14 2.87505 1.8723005E+04 1.0450857E+07 558.18 2.90005 1.8704799E+04 1.0441382E+07 558.22 2.92505 1.8678392E+04 1.0427269E+07 558.25 2.95003 1.8650919E+04 1.0412569E+07 558.29 2.97508 1.8627102E+04 1.0399953E+07 558.32 3.00020 1.8605296E+04 1.0388476E+07 558.36 6.2.1-122 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-31 Reactor Cavity Volumes (Page 1 of 2) | |||
COMPARTMENT NUMBER COMPARTMENT LOCATION VOLUME (ft3) 1 Break Location 164.595 2 Lower Reactor Cavity 12,000. | |||
3 Reactor Vessel Annulus 1.319 4 Reactor Vessel Annulus 1.938 5 Reactor Vessel Annulus 8.601 6 Reactor Vessel Annulus 8.601 7 Reactor Vessel Annulus 9.825 8 Reactor Vessel Annulus 17.202 9 Reactor Vessel Annulus 9.825 10 Reactor Vessel Annulus 17.202 11 Reactor Vessel Annulus 9.205 12 Reactor Vessel Annulus 17.202 13 Reactor Vessel Annulus 9.206 14 Reactor Vessel Annulus 17.202 15 Reactor Vessel Annulus 9.825 16 Reactor Vessel Annulus 17.202 17 Reactor Vessel Annulus 9.825 18 Reactor Vessel Annulus 17.202 19 Reactor Vessel Annulus 9.206 20 Reactor Vessel Annulus 17.202 21 Lower Containment 60,000. | |||
22 Lower Containment 60,000. | |||
23 Lower Containment 60,000. | |||
24 Lower Containment 60,000. | |||
25 Break Location 165.206 26 Inspection Annulus 165.819 27 Inspection Annulus 165.206 28 Inspection Annulus 164.595 29 Inspection Annulus 165.206 30 Inspection Annulus 165.819 31 Inspection Annulus 165.206 32 Upper Containment 651,000. | |||
33 Reactor Vessel Annulus 1.404 34 Reactor Vessel Annulus 1.404 35 Reactor Vessel Annulus 1.938 36 Reactor Vessel Annulus 8.601 37 Reactor Vessel Annulus 8.601 38 Reactor Vessel Annulus 17.202 39 Reactor Vessel Annulus 17.202 40 Reactor Vessel Annulus 17.202 41 Reactor Vessel Annulus 17.202 42 Reactor Vessel Annulus 17.202 43 Reactor Vessel Annulus 17.202 44 Reactor Vessel Annulus 17.202 45 Reactor Vessel Annulus 0.602 46 Reactor Vessel Annulus 0.602 47 Upper Reactor Cavity 15,500. | |||
48 Ice Condenser 24,241. | |||
Containment Functional Design 6.2.1-123 | |||
WATTS BAR WBNP-112 Table 6.2.1-31 Reactor Cavity Volumes (Page 2 of 2) | |||
COMPARTMENT NUMBER COMPARTMENT LOCATION VOLUME (ft3) 49 Ice Condenser 28,760. | |||
50 Ice Condenser 28,760. | |||
51 Ice Condenser 28,760. | |||
52 Ice Condenser 47,000. | |||
53 Pipe Annulus 150. | |||
54 Inspection Port 17.280 55 Inspection Port 17.280 56 Inspection Port 17.280 57 Inspection Port 17.280 58 Inspection Port 17.280 59 Inspection Port 17.280 60 Inspection Port 17.280 61 Inspection Port 17.280 62 Pipe Annulus 47. | |||
63 Pipe Annulus 47. | |||
64 Pipe Annulus 47. | |||
65 Pipe Annulus 47. | |||
66 Pipe Annulus 47. | |||
67 Pipe Annulus 47. | |||
68 Pipe Annulus 150. | |||
6.2.1-124 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-32 Flow Path Data (Reactor Cavity) (Page 1 of 3) | |||
Inertia Hydraulic Flow Equiv. Area Length Diameter Area Length Ratio Between Compartments k f (ft) (ft) (ft2) (ft) a/A 1 to 3 0.4 0.02 1.6 0.3 2.7 1.2 0.28 2 to 22 2.9 0.02 28. 5.8 36. 19. 0.0 3 to 34 1.0 0.02 0.7 0.4 1.2 0.7 1.0 4 to 35 0.0 0.02 3.6 0.4 0.7 3.6 1.0 5 to 36 0.0 0.02 3.3 0.4 2.6 3.3 1.0 6 to 37 0.0 0.02 3.3 0.4 2.6 3.3 1.0 7 to 9 1.0 0.02 4.9 0.4 1.0 4.1 1.0 8 to 10 0.0 0.02 6.6 0.4 2.6 6.6 1.0 9 to 11 1.04 0.02 4.6 0.4 1.0 3.7 0.46 10 to 12 0.0 0.02 6.6 0.4 2.6 6.6 1.0 11 to 13 1.04 0.02 4.8 0.4 1.0 4.0 0.46 12 to 14 0.0 0.02 6.6 0.4 2.6 6.6 1.0 13 to 15 1.04 0.02 4.6 0.4 1.0 3.7 0.46 14 to 16 0.0 0.02 6.6 0.4 2.6 6.6 1.0 15 to 17 1.04 0.02 4.9 0.4 1.0 4.1 0.5 16 to 18 0.0 0.02 6.6 0.4 2.6 6.6 1.0 17 to 19 1.0 0.02 4.6 0.4 1.0 3.7 0.46 18 to 20 0.0 0.02 6.6 0.4 2.6 6.6 1.0 19 to 4 1.0 0.02 5.4 0.4 0.5 5.4 1.0 20 to 6 0.0 0.02 5.0 0.4 2.6 5.0 1.0 21 to 22 2.0 0.02 38. 40. 1560. 38. 0.43 22 to 23 3.0 0.02 38. 40. 1560. 38. 0.47 23 to 24 2.0 0.02 38. 40. 1560. 38. 0.43 24 to 21 3.0 0.02 32. 8.0 100. 27. 0.09 25 to 7 2.8 0.02 3.0 0.2 1.1 1.7 0.12 26 to 9 2.8 0.02 3.0 0.2 1.1 1.7 0.12 27 to 11 2.8 0.02 3.1 0.2 1.3 1.7 0.13 28 to 13 2.8 0.02 3.1 0.2 1.3 1.7 0.13 29 to 15 2.8 0.02 3.0 0.2 1.1 1.7 0.12 30 to 17 2.8 0.02 3.0 0.2 1.1 1.7 0.12 31 to 19 2.8 0.02 3.1 0.2 1.3 1.7 0.13 33 to 3 1.0 0.02 0.7 0.4 1.2 0.7 0.99 34 to 7 1.0 0.02 3.6 0.4 1.2 3.3 0.66 35 to 7 1.0 0.02 5.4 0.4 0.5 5.4 1.0 36 to 38 0.0 0.02 5.0 0.4 2.2 5.0 1.0 37 to 8 0.0 0.02 5.0 0.4 2.6 5.0 1.0 38 to 39 0.0 0.02 6.6 0.4 2.6 6.6 1.0 39 to 40 0.0 0.02 6.6 0.4 2.6 6.6 1.0 40 to 41 0.0 0.02 6.6 0.4 2.6 6.6 1.0 41 to 42 0.0 0.02 6.6 0.4 2.6 6.6 1.0 42 to 43 0.0 0.02 6.6 0.4 2.6 6.6 1.0 43 to 44 0.0 0.02 6.6 0.4 2.6 6.6 1.0 44 to 5 0.0 0.02 5.0 0.4 2.6 5.0 1.0 45 to 3 1.0 0.02 0.8 0.4 0.5 0.8 0.78 46 to 3 1.0 0.02 0.8 0.4 0.5 0.8 0.78 53 to 1 0.4 0.02 7.6 0.83 5.5 6.8 0.11 54 to 1 0.5 0.02 2.6 2.5 4.9 1.9 0.25 55 to 25 0.5 0.02 2.6 2.5 4.9 1.9 0.25 56 to 26 0.5 0.02 2.6 2.5 4.9 2.0 0.26 Containment Functional Design 6.2.1-125 | |||
WATTS BAR WBNP-112 Table 6.2.1-32 Flow Path Data (Reactor Cavity) (Page 2 of 3) | |||
Inertia Hydraulic Flow Equiv. Area Length Diameter Area Length Ratio Between Compartments k f (ft) (ft) (ft2) (ft) a/A 57 to 27 0.5 0.02 2.6 2.5 4.9 1.9 0.25 58 to 28 0.5 0.02 2.6 2.5 4.9 1.9 0.25 59 to 29 0.5 0.02 2.6 2.5 4.9 1.9 0.25 60 to 30 0.5 0.02 2.6 2.5 4.9 2.0 0.26 61 to 31 0.5 0.02 2.6 2.5 4.9 1.9 0.25 62 to 25 0.4 0.02 3.0 0.83 5.5 2.2 0.11 63 to 26 0.4 0.02 3.0 0.83 5.5 2.2 0.11 64 to 27 0.4 0.02 3.0 0.83 5.5 2.2 0.11 65 to 28 0.4 0.02 3.0 0.83 5.5 2.2 0.11 66 to 29 0.4 0.02 3.0 0.83 5.5 2.2 0.11 67 to 30 0.4 0.02 3.0 0.83 5.5 2.2 0.11 68 to 31 0.4 0.02 7.6 0.83 5.5 6.8 0.11 1 to 19 0.4 0.02 3.1 0.2 1.3 1.7 0.13 2 to 6 3.7 0.02 6.5 0.4 0.7 6.4 0.0 4 to 45 0.6 0.02 2.4 0.4 0.7 2.4 0.95 6 to 5 0.0 0.02 13. 0.4 0.7 13. 1.0 7 to 38 1.0 0.02 6.0 0.4 0.3 4.7 0.23 8 to 2 3.7 0.02 6.6 0.4 1.3 6.4 0.0 9 to 39 9.2 0.02 6.7 0.4 0.3 4.9 0.23 10 to 2 3.7 0.02 6.6 0.4 1.3 6.4 0.0 11 to 40 1.0 0.02 5.5 0.4 0.2 4.5 0.17 12 to 2 3.7 0.02 6.6 0.4 1.3 6.4 0.0 13 to 41 9.2 0.02 6.0 0.4 0.2 4.6 0.17 14 to 2 3.7 0.02 6.6 0.4 1.3 6.4 0.0 15 to 42 1.0 0.02 6.0 0.4 0.3 4.7 0.23 16 to 2 3.7 0.02 6.6 0.4 1.3 6.4 0.0 17 to 43 9.2 0.02 6.7 0.4 0.3 4.9 0.23 18 to 2 3.7 0.02 6.6 0.4 1.3 6.4 0.0 19 to 44 1.0 0.02 5.5 0.4 0.2 4.5 0.17 20 to 2 3.7 0.02 6.6 0.4 1.3 6.4 0.0 21 to 48 .7837 0.0 10.36 1.0 265.875 0.0 0.096 22 to 48 .7837 0.0 10.36 1.0 265.875 0.0 0.096 23 to 48 .7837 0.0 10.36 1.0 265.875 0.0 0.096 24 to 48 .7837 0.0 10.36 1.0 265.875 0.0 0.096 25 to 3 0.4 0.02 1.6 0.3 2.7 1.2 0.28 26 to 7 0.4 0.02 3.0 0.2 1.1 1.7 0.12 27 to 9 0.4 0.02 3.0 0.2 1.1 1.7 0.12 28 to 11 0.4 0.02 3.1 0.2 1.3 1.7 0.13 29 to 13 0.4 0.02 3.1 0.2 1.3 1.7 0.13 30 to 15 0.4 0.02 3.0 0.2 1.1 1.7 0.12 31 to 17 0.4 0.02 3.0 0.2 1.1 1.7 0.12 33 to 46 2.2 0.02 3.3 0.4 0.4 3.3 0.25 34 to 46 2.2 0.02 3.3 0.4 0.4 3.3 0.25 35 to 47 1.1 0.02 3.0 0.4 0.7 1.5 0.0 37 to 36 0.0 0.02 13. 0.4 0.7 13. 1.0 38 to 8 0.0 0.02 13. 0.4 1.3 13. 1.0 39 to 10 0.0 0.02 13. 0.4 1.3 13. 1.0 6.2.1-126 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-32 Flow Path Data (Reactor Cavity) (Page 3 of 3) | |||
Inertia Hydraulic Flow Equiv. Area Length Diameter Area Length Ratio Between Compartments k f (ft) (ft) (ft2) (ft) a/A 40 to 12 0.0 0.02 13. 0.4 1.3 13. 1.0 41 to 14 0.0 0.02 13. 0.4 1.3 13. 1.0 42 to 16 0.0 0.02 13. 0.4 1.3 13. 1.0 43 to 18 0.0 0.02 13. 0.4 1.3 13. 1.0 44 to 20 0.0 0.02 13. 0.4 1.3 13. 1.0 45 to 33 0.0 0.02 3.3 0.4 0.4 3.3 0.25 48 to 49 0.0 0.1055 8.733 0.855 989.01 8.0 0.230 49 to 50 0.0 0.0592 12.278 0.855 982.47 16.0 0.239 50 to 51 0.0 0.0592 12.278 0.855 982.47 16.0 0.359 51 to 52 0.87979 0.1249 8.8558 0.855 982.47 8.0 0.359 52 to 32 1.43 0.0 2.8 1.0 2003.1 0.269 53 to 25 0.4 0.02 7.6 0.83 5.5 6.8 0.11 54 to 47 1.0 0.02 1.9 2.5 4.9 1.8 0.0 55 to 47 1.0 0.02 1.9 2.5 4.9 1.8 0.0 56 to 47 1.0 0.02 1.9 2.5 4.9 1.8 0.0 57 to 47 1.0 0.02 1.9 2.5 4.9 1.8 0.0 58 to 47 1.0 0.02 1.9 2.5 4.9 1.8 0.0 59 to 47 1.0 0.02 1.9 2.5 4.9 1.8 0.0 60 to 47 1.0 0.02 1.9 2.5 4.9 1.8 0.0 61 to 47 1.0 0.02 1.9 2.5 4.9 1.8 0.0 62 to 26 0.4 0.02 3.0 0.83 5.5 2.2 0.11 63 to 27 0.4 0.02 3.0 0.83 5.5 2.2 0.11 64 to 28 0.4 0.02 3.0 0.83 5.5 2.2 0.11 65 to 29 0.4 0.02 3.0 0.83 5.5 2.2 0.11 66 to 30 0.4 0.02 3.0 0.83 5.5 2.2 0.11 67 to 31 0.4 0.02 3.0 0.83 5.5 2.2 0.11 68 to 1 0.4 0.02 7.6 0.83 5.5 8.8 0.11 1 to 25 1.0 0.02 5.4 1.5 9.6 2.6 0.47 2 to 37 3.7 0.02 6.5 0.4 0.7 6.4 0.0 4 to 47 1.1 0.02 3.0 0.4 0.7 1.5 1.0 5 to 46 9.2 0.02 7.8 2.0 0.5 18. 1.0 7 to 47 1.1 0.02 3.0 0.4 1.4 2.9 0.0 9 to 47 1.1 0.02 3.0 0.4 1.4 2.9 0.0 11 to 47 1.1 0.02 3.0 0.4 1.4 2.9 0.0 13 to 47 1.1 0.02 3.0 0.4 1.4 2.9 0.0 15 to 47 1.1 0.02 3.0 0.4 1.4 2.9 0.0 17 to 47 1.1 0.02 3.0 0.4 1.4 2.9 0.0 19 to 47 1.1 0.02 3.0 0.4 1.4 2.9 0.0 21 to 47 3.8 0.02 5.8 5.1 26. 4.0 0.04 22 to 47 3.8 0.02 9.1 12. 74. 4.2 0.10 23 to 47 3.8 0.02 8.3 11. 62. 4.0 0.08 24 to 47 3.9 0.02 6.3 5.5 32. 4.0 0.04 25 to 26 1.0 0.02 5.3 1.4 9.1 2.3 0.44 26 to 27 1.0 0.02 5.3 1.4 9.1 2.6 0.44 27 to 28 1.0 0.02 5.4 1.5 9.6 2.6 0.47 28 to 29 1.0 0.02 5.4 1.5 9.6 2.6 0.47 29 to 30 1.0 0.02 5.3 1.4 9.1 2.6 0.44 30 to 31 1.0 0.02 5.3 1.4 9.1 2.6 0.44 31 to 1 1.0 0.02 5.4 1.5 9.6 2.6 0.47 33 to 19 1.0 0.02 3.6 0.4 1.2 3.3 0.61 35 to 46 0.6 0.02 2.4 0.4 0.7 2.4 0.95 36 to 46 9.2 0.02 7.8 2.0 0.5 18. 0.95 45 to 34 0.0 0.02 3.3 0.4 0.4 3.3 0.25 53 to 21 1.0 0.02 7.2 17. 11.0 8.8 0.0 62 to 21 1.0 0.02 2.5 1.5 11.0 2.1 0.0 63 to 22 1.0 0.02 2.5 1.5 11.0 2.1 0.0 64 to 22 1.0 0.02 2.5 1.7 11.0 2.1 0.0 65 to 23 1.0 0.02 2.5 1.7 11.0 2.1 0.0 66 to 23 1.0 0.02 2.5 1.5 11.0 2.1 0.0 67 to 24 1.0 0.02 2.5 1.5 11.0 2.1 0.0 68 to 24 1.0 0.02 7.2 1.7 11.0 6.8 0.0 Containment Functional Design 6.2.1-127 | |||
WATTS BAR WBNP-112 Table 6.2.1-33 Containment Data (ECCS Analysis) | |||
(Page 1 of 2) | |||
I. Conservatively High Estimate of Containment Net Free Volume Containment Area Volume (ft3) | |||
Upper Compartment 651,000 Lower Compartment 271,400 Ice Condenser 169,400 Dead-Ended Compartments (includes all accumulator rooms, both 129,900 fan compartments, instrument room pipe tunnel) | |||
II. Initial Conditions A. Containment Pressure 15.0 psia B. Lowest Operational Containment Temperature for the Upper, 85°F Lower, and Dead-Ended Compartments 100°F C. Highest Refueling Water Storage Tank Temperature 100°F D. Lowest Temperature Outside Containment 5°F E. Highest Initial Spray Temperature 100°F F. Lowest Annulus Temperature 40°F III. Structural Heat Sinks** | |||
A. For Each Surface | |||
: 1. Description of Surface | |||
: 2. Conservatively High Estimate of Area Exposed to Containment See Tables 6.2.1-34 Atmosphere through 6.2.1-36 | |||
: 3. Location in Containment by Compartment B. For Each Separate Layer of Each Surface | |||
: 1. Material | |||
: 2. Conservatively Large Estimate of Layer Thickness See Tables 6.2.1-34 through 6.2.1-36 | |||
: 3. Conservatively High Value of Material Conductivity See Tables 6.2.1-34 through 6.2.1-36 | |||
: 4. Conservatively High Value of Volumetric Heat Capacity See Tables 6.2.1-34 through 6.2.1-36 6.2.1-128 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-33 Containment Data (ECCS Analysis) | |||
(Page 2 of 2) | |||
IV. Spray System A. Runout Flow for a Spray Pump*** (Containment Spray) 7700 gpm B. Number of Spray Pumps Operating with No Diesel Failure 2/Unit C. Number of Spray Pumps Operating with One Diesel Failure 1/Unit D. Assumed Post Accident Initiation of Spray System 25 sec V. Deck Fan A. Fastest Post Accident Initiation of Deck Fans 10 min B. Conservatively High Flow Rate Per Fan 42,000 cfm VI. Conservatively Low Hydrogen Skimmer System Flow Rate 100 cfm/each | |||
** Structural heat sinks should also account for any surfaces neglected in containment integrity analysis. | |||
*** Runout flow is for a break immediately downstream of the pump. In that event, the spray water will not enter the containment. | |||
Containment Functional Design 6.2.1-129 | |||
WATTS BAR WBNP-112 Table 6.2.1-34 Major Characteristics Of Structural Heat Sinks Inside Sequoyah Nuclear Plant Containment - Upper Compartment Heat Thickness Volume Transfer and Thermal Heat Area Material Conductivity Capacity Structure (ft2) (as noted) (Btu/ft-hr-°F) (Btu/ft3-°F) | |||
Operating Deck 4,452 1.1 ft concrete 0.84 30.24 7,749 6.3 mils coating 0.087 29.8 1.1 ft concrete 0.84 30.24 672 1.6 ft concrete 0.84 30.24 11,445 6.3 mils coating 0.087 29.8 1.6 ft concrete 0.84 30.24 4,032 0.26 in. stainless steel 9.87 59.22 1.6 ft concrete 0.84 30.24 798 15.7 mils coating 0.087 29.8 1.6 ft concrete 0.84 30.24 Containment Shell 22,890 7.8 mils coating 0.21 29.8 0.46 in. carbon steel 27.3 30.24 18,375 7.8 mils coating 0.21 29.8 0.58 in. carbon steel 27.3 59.22 2,100 7.8 mils coating 0.21 29.8 1.51 in. carbon steel 27.3 59.22 Miscellaneous Steel 4,095 7.8 mils coating 0.21 29.8 0.26 in. carbon steel 27.3 59.22 3,559 7.8 mils coating 0.21 29.8 0.46 in. carbon steel 27.3 59.22 3,539 7.8 mils coating 0.21 29.8 0.72 in. carbon steel 27.3 59.22 273 7.8 mils coating 0.21 29.8 1.57 in. carbon steel 27.3 59.2 6.2.1-130 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-35 Major Characteristics Of Structural Heat Sinks Inside Sequoyah Nuclear Plant Containment - Lower Compartment (Page 1 of 2) | |||
Heat Thickness Volume Transfer and Thermal Heat Area Material Conductivity Capacity Structure (ft2) (as noted) (Btu/ft-hr-°F) (Btu/ft3-°F) | |||
Operating Deck 7,507 1.1 ft concrete 0.84 30.24 2,971 1.6 mils coating 0.087 29.8 1.1 ft concrete 0.84 30.24 2,131 1.6 ft concrete 0.84 30.24 789 6.3 mils coating 0.087 29.8 1.84 ft concrete 0.84 30.24 2,646 2.1 ft concrete 0.84 30.24 210 6.3 mils coating 0.087 29.8 2.1 ft concrete 0.84 30.24 Crane Wall 14,752 1.6 ft concrete 0.84 30.24 3,570 6.3 mils coating 0.087 29.8 1.6 ft concrete 0.84 30.24 Containment Floor 567 1.6 ft concrete 0.84 30.24 7,612 6.3 mils coating 0.087 29.8 1.6 ft concrete 0.84 30.24 Interior Concrete 3,780 1.1 ft concrete 0.84 30.24 567 1.1 ft concrete 0.84 30.24 2,992 2.1 ft concrete 0.84 30.24 2,384 0.26 in. stainless 9.8 59.2 steel 2.1 ft concrete 0.84 30.24 2,373 2.1 ft concrete 0.84 30.24 1,480 6.3 mils coating 0.087 29.8 2.1 ft concrete 0.84 30.24 Miscellaneous Steel 12,915 7.8 mils coating 0.22 14.7 0.53 in. carbon steel 27.3 59.2 7,560 7.8 mils coating 0.22 14.7 0.78 in. carbon steel 27.3 59.2 5,250 7.8 mils coating 0.22 14.7 1.1 carbon steel 27.3 59.2 Containment Functional Design 6.2.1-131 | |||
WATTS BAR WBNP-112 Table 6.2.1-35 Major Characteristics Of Structural Heat Sinks Inside Sequoyah Nuclear Plant Containment - Lower Compartment (Page 2 of 2) | |||
Heat Thickness Volume Transfer and Thermal Heat Area Material Conductivity Capacity Structure (ft2) (as noted) (Btu/ft-hr-°F) (Btu/ft3-°F) 2,625 7.8 mils coating 0.22 14.7 1.45 in. carbon steel 27.3 59.2 1,575 7.8 mils coating 0.22 14.7 1.7 in. carbon steel 27.3 59.2 6.2.1-132 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-36 Major Characteristics Of Structural Heat Sinks Inside Sequoyah Nuclear Plant Containment - Dead-Ended Compartment Heat Thickness and Thermal Volume Heat Transfer Material (as noted) Conductivity (Btu/ft- Capacity Structure Area (ft2) hr-°F) (Btu/ft3-°F) | |||
Containment Shell 3,045 7.8 mils coating 0.22 14.7 0.78 in. carbon steel 27.3 59.2 4,305 7.8 mils coating 0.22 14.7 1.1 in. carbon steel 27.3 59.2 4,305 7.8 mils coating 0.22 14.7 1.25 in. carbon steel 27.3 59.2 3,780 7.8 mils coating 0.22 14.7 1.37 in. carbon steel 27.3 59.2 4,305 7.8 mils coating 0.22 14.7 1.51 in. carbon steel 27.3 59.2 Crane Wall 7,255 1.6 ft concrete 0.84 30.24 3,801 6.3 mils coating 0.87 14.7 1.58 ft concrete 0.84 30.24 Containment Floor 4,809 6.3 mils coating 0.087 14.7 2.1 ft concrete 0.84 30.24 Interior Concrete 9,870 1.1 ft concrete 0.84 30.24 3,948 6.3 mils coating 0.087 14.7 1.1 ft concrete 0.84 30.24 5,376 1.58 ft concrete 0.84 30.24 Containment Functional Design 6.2.1-133 | |||
WATTS BAR WBNP-112 Table 6.2.1-37 Maximum Reverse Pressure Differential Pressure Analysis Base Case Westinghouse ECCS structural heat transfer model Sprays at runout flow Offsite power available spray start time Minimum containment temperature Dead-ended volume is swept Max. reverse differential pressure = 0.65 psi Case Variable Change in Max. dP (psi) 1 Ice condenser flow through the drains acts as 50% thermal +0.2 efficient spray 2 Same as Case 1, except 100% thermal efficiency +0.4 3 Maximum containment temperature -0.2 4 Heat transfer coefficient to sump equals 5 times Hmax <0.1 5 Same as Case 2, except drain flow rate times 1.5 +0.6 6 Combination of Cases 2 and 4 +0.4 7 1 bay of ice condenser doors remains open -0.65 8 Same as Case 6 except Equation (3) written as +0.55 H = Hstag + [Hmax - Hstag] e-.025 [t-tp] | |||
9 Same as Case 6 except 5 times upper to lower resistance +2.0 10 RWST temperature = 105°F +0.2 6.2.1-134 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-38 Ice Condenser Steam Exit Flow vs. Time vs. Sump Temperature (Page 1 of 3) | |||
Ice Condenser Steam Exit Flow Time (sec) Sump Temp. (°F) (lb/sec) 13.1 190.3 -1.74 13.8 190.6 -1.63 14.4 190.7 -1.76 15.0 190.9 -1.54 15.4 191.1 -1.37 15.9 191.2 -1.23 16.3 191.3 -.13 16.6 191.4 -.09 17.0 191.5 -.09 17.4 191.6 -.08 17.8 191.7 -.08 18.2 191.8 -.07 18.6 191.9 -.07 19.0 192.0 -.07 19.3 192.1 -.07 19.7 192.2 -.06 20.0 192.3 -1.04 20.3 192.4 -.93 20.9 192.5 -1.17 21.5 192.7 -1.43 21.8 192.8 -2.24 22.4 192.9 -2.95 23.0 193.1 -2.85 23.6 193.2 -2.64 23.9 193.3 -2.53 24.5 193.4 -2.34 25.1 193.8 -2.17 25.4 194.0 -2.05 25.7 194.1 -1.94 26.0 194.2 -1.85 Containment Functional Design 6.2.1-135 | |||
WATTS BAR WBNP-112 Table 6.2.1-38 Ice Condenser Steam Exit Flow vs. Time vs. Sump Temperature (Page 2 of 3) | |||
Ice Condenser Steam Exit Flow Time (sec) Sump Temp. (°F) (lb/sec) 26.6 194.6 -1.69 27.2 194.8 -1.58 27.5 194.9 -1.53 28.0 195.2 -1.45 29.5 195.6 -1.40 30.1 195.8 -1.42 30.7 196.0 -1.44 31.3 196.2 -1.45 31.9 196.3 -1.45 32.5 196.4 -1.43 33.1 196.5 -1.40 33.7 196.6 -1.36 34.3 196.8 -1.31 34.9 196.9 -1.26 35.5 196.9 -1.20 36.0 197.0 -1.115 36.9 197.2 -0.96 37.9 197.3 -0.80 38.9 197.4 -0.63 40.1 197.4 -0.44 41.3 197.5 -0.29 42.2 197.5 -0.20 44.0 197.4 -.09 44.9 197.3 -0.4 45.4 197.3 .12 46.7 197.2 .19 47.6 197.0 .20 48.9 196.9 .19 49.8 196.7 .17 51.2 196.5 .12 6.2.1-136 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-38 Ice Condenser Steam Exit Flow vs. Time vs. Sump Temperature (Page 3 of 3) | |||
Ice Condenser Steam Exit Flow Time (sec) Sump Temp. (°F) (lb/sec) 52.3 196.4 .07 53.6 196.1 .01 54.4 196.0 -.01 55.2 195.9 -.03 56.2 195.7 -.05 57.1 195.5 -.07 58.0 195.4 -.10 59.0 195.2 -.17 59.9 195.0 -.14 60.9 194.9 -.15 61.6 194.7 -.17 62.8 194.5 -.18 63.7 194.3 -.20 64.7 194.2 -.22 65.6 194.0 -.24 66.6 193.8 -.31 67.5 193.6 -.41 68.4 193.5 -.60 69.4 193.3 .20 70.3 193.2 .63 71.3 193.0 .84 72.2 192.9 1.05 73.2 192.7 1.25 74.1 192.6 1.39 75.1 192.5 1.54 76.0 192.4 1.66 77.0 192.3 1.78 Containment Functional Design 6.2.1-137 | |||
WATTS BAR WBNP-112 t | |||
Table 6.2.1-39 Mass and Energy Release Rates For Specified Steam Line Breaks I. Run 1 - 1.4 ft² Break, 100.6% Power, AFW Runout Protection Failure Mass Flow Rate Energy Flow Rate Time (sec) (lbm/sec) (Btu/sec) 0.01 12704.8 15143070.0 0.6 12618.8 15043683.0 1.00 12553.8 14969156.0 2.0 12405.8 14798220.0 3.0 12272.8 14642025.0 4.0 11312.0 13487580.0 5.0 10363.0 12391015.0 6.0 9590.0 11481560.0 7.0 9215.0 11041828.0 8.2 8940.0 10721244.0 8.4 8896.0 10668477.0 10.0 8594.0 10314893.0 11.0 8408.0 10091639.0 12.0 8203.0 9853781.0 12.4 8112.0 9744465.0 12.6 1940.0 2331880.0 14.0 1846.0 2218892.0 17.6 1624.0 1955296.0 20.0 1502.0 1808408.0 25.2 1310.0 1577240.0 30.2 1177.0 1417108.0 35.2 1082.0 1302728.0 45.20 970.3 1168241.0 60.2 887.7 1067903.0 90.2 812.5 976625.0 150.2 760.3 913880.6 200.2 746.5 897293.0 250.2 730.7 877570.7 300.2 615.1 737504.9 312.2 515.7 617292.9 6.2.1-138 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-39 Mass and Energy Release Rates For Specified Steam Line Breaks I. Run 1 - 1.4 ft² Break, 100.6% Power, AFW Runout Protection Failure Mass Flow Rate Energy Flow Rate Time (sec) (lbm/sec) (Btu/sec) 326.2 416.4 496765.2 368.2 315.0 374220.0 420.2 308.6 366616.8 500.2 308.1 366022.8 600.2 307.9 365785.2 604.2 329.1 391299.9 606.2 223.5 264177.0 612.2 116.9 136656.1 622.2 58.11 67175.16 700.2 0.0 0.0 Containment Functional Design 6.2.1-139 | |||
WATTS BAR WBNP-112 Table 6.2.1-39 Mass and Energy Release Rates For Specified Steam Line Breaks (Contd) | |||
II. Run 2 - 0.6 ft² Split, 30% Power, AFW Runout Protection Failure Mass Flow Rate Energy Flow Rate Time (sec) (lbm/sec) (Btu/sec) | |||
.1000E-01 .1375E+04 .1633E+07 | |||
.6000E+00 .1371E+04 .1628E+07 | |||
.1000E+01 .1363E+04 .1619E+07 | |||
.2000E+01 .1345E+04 .1599E+07 | |||
.3000E+01 .1330E+04 .1581E+07 | |||
.4000E+01 .1315E+04 .1564E+07 | |||
.5000E+01 .1300E+04 .1547E+07 | |||
.5400E+01 .1295E+04 .1541E+07 | |||
.6000E+01 .1300E+04 .1547E+07 | |||
.7000E+01 .1299E+04 .1546E+07 | |||
.8000E+01 .1299E+04 .1545E+07 | |||
.1220E+02 .1296E+04 .1542E+07 | |||
.1400E+02 .1292E+04 .1538E+07 | |||
.1600E+02 .1251E+04 .1491E+07 | |||
.1800E+02 .1178E+04 .1407E+07 | |||
.2000E+02 .1116E+04 .1335E+07 | |||
.2420E+02 .1018E+04 .1220E+07 | |||
.2820E+02 .9426E+03 .1131E+07 | |||
.3220E+02 .8813E+03 .1058E+07 | |||
.3620E+02 .8309E+03 .9986E+06 | |||
.4020E+02 .7886E+03 .9483E+06 | |||
.4420E+02 .7533E+03 .9063E+06 | |||
.4620E+02 .7376E+03 .8876E+06 | |||
.4820E+02 .7231E+03 .8702E+06 | |||
.5020E+02 .7095E+03 .8540E+06 | |||
.5420E+02 .6851E+03 .8248E+06 | |||
.5870E+02 .6612E+03 .7961E+06 | |||
.6620E+02 .6278E+03 .7561E+06 | |||
.7220E+02 .6056E+03 .7293E+06 | |||
.8820E+02 .5600E+03 .6745E+06 6.2.1-140 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-39 Mass and Energy Release Rates For Specified Steam Line Breaks (Contd) | |||
II. Run 2 - 0.6 ft² Split, 30% Power, AFW Runout Protection Failure Mass Flow Rate Energy Flow Rate Time (sec) (lbm/sec) (Btu/sec) | |||
.9920E+02 .5368E+03 .6465E+06 | |||
.1162E+03 .5149E+03 .6201E+06 | |||
.1342E+03 .4912E+03 .5916E+06 | |||
.2042E+03 .4186E+03 .5039E+06 | |||
.3042E+03 .3738E+03 .4497E+06 | |||
.4102E+03 .3229E+03 .3881E+06 | |||
.5122E+03 .2721E+03 .3265E+06 | |||
.6022E+03 .2348E+03 .2812E+06 | |||
.6242E+03 .2443E+03 .2928E+06 | |||
.7002E+03 .2300E+03 .2754E+06 Containment Functional Design 6.2.1-141 | |||
WATTS BAR WBNP-112 Table 6.2.1-39 Mass and Energy Release Rates For Specified Steam Line Breaks (Contd) | |||
III. Run 3 - 0.35 ft² Split, 30% Power, AFW Runout Protection Failure Mass Flow Rate Energy Flow Rate Time (sec) (lbm/sec) (Btu/sec) | |||
.1000E-01 .8057E+03 .9565E+06 | |||
.6000E+00 .8041E+03 .9548E+06 | |||
.1000E+01 .8013E+03 .9516E+06 | |||
.2000E+01 .7953E+03 .9447E+06 | |||
.3000E+01 .7897E+03 .9383E+06 | |||
.4000E+01 .7845E+03 .9324E+06 | |||
.6000E+01 .7752E+03 .9217E+06 | |||
.8000E+01 .7664E+03 .9115E+06 | |||
.1000E+02 .7736E+03 .9199E+06 | |||
.1580E+02 .7857E+03 .9338E+06 | |||
.2000E+02 .7789E+03 .9260E+06 | |||
.2220E+02 .7501E+03 .8931E+06 | |||
.2320E+02 .7358E+03 .8766E+06 | |||
.2420E+02 .7227E+03 .8615E+06 | |||
.2520E+02 .7105E+03 .8474E+06 | |||
.2670E+02 .6937E+03 .8279E+06 | |||
.2820E+02 .6783E+03 .8101E+06 | |||
.2920E+02 .6688E+03 .7990E+06 | |||
.3270E+02 .6386E+03 .7639E+06 | |||
.3570E+02 .6161E+03 .7375E+06 | |||
.3970E+02 .5900E+03 .7069E+06 | |||
.4420E+02 .5647E+03 .6771E+06 | |||
.4920E+02 .5410E+03 .6492E+06 | |||
.5570E+02 .5157E+03 .6192E+06 | |||
.6320E+02 .4917E+03 .5909E+06 | |||
.7270E+02 .4673E+03 .5618E+06 | |||
.8420E+02 .4437E+03 .5338E+06 | |||
.9920E+02 .4197E+03 .5051E+06 | |||
.1182E+03 .3969E+03 .4779E+06 | |||
.1442E+03 .3727E+03 .4489E+06 6.2.1-142 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-39 Mass and Energy Release Rates For Specified Steam Line Breaks (Contd) | |||
III. Run 3 - 0.35 ft² Split, 30% Power, AFW Runout Protection Failure Mass Flow Rate Energy Flow Rate Time (sec) (lbm/sec) (Btu/sec) | |||
.1792E+03 .3500E+03 .4216E+06 | |||
.2222E+03 .3254E+03 .3919E+06 | |||
.2662E+03 .3004E+03 .3619E+06 | |||
.3182E+03 .2752E+03 .3314E+06 | |||
.3782E+03 .2513E+03 .3026E+06 | |||
.4542E+03 .2277E+03 .2740E+06 | |||
.5422E+03 .2029E+03 .2439E+06 | |||
.6022E+03 .1877E+03 .2255E+06 | |||
.6382E+03 .1955E+03 .2350E+06 | |||
.7002E+03 .1904E+03 .2288E+06 Containment Functional Design 6.2.1-143 | |||
WATTS BAR WBNP-112 t | |||
Table 6.2.1-40 Steam Line Break Cases For Core Integrity Boric Acid Concentration Case Type of Break (ppm) 1 Hypothetical with offsite power, downstream of the flow restrictor 0 2 Hypothetical without offsite power, downstream of the flow 0 restrictor 3 Credible - Uniform 0 4 Credible - Nonuniform 0 6.2.1-144 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-41 Line Break(1) Descriptions For Mass And Energy Releases 100.6% Power - AFW Pump Runout Protection Failure 100.6% Power - Feed Control Valve (FCV) Failure 100.6% Power - No Failure 100.6% Power - Feedwater Isolation Valve (FWIV) Failure 0% Power - AFW Pump Runout Protection Failure 0% Power - Feed Control Valve (FCV) Failure 0% Power - No Failure 0% Power - Feedwater Isolation Valve (FWIV) Failure Notes: | |||
(1) For 1.4 ft2 break Containment Functional Design 6.2.1-145 | |||
WATTS BAR WBNP-112 Table 6.2.1-42 Small Break Descriptions For Mass And Energy Break Size (ft2) Description 0.944 30% Power - AFW Pump Runout Protection Failure 0.6 30% Power - AFW Pump Runout Protection Failure 0.35 30% Power - AFW Pump Runout Protection Failure 0.1 30% Power - AFW Pump Runout Protection Failure 0.86 100.6% Power - AFW Pump Runout Protection Failure 6.2.1-146 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-43 Large Break Analysis - Associated Times Maximum Lower Compartment Time, Tmax Case Temperature (°F) (sec) 1.4 ft2, 100.6% Power - AFW Pump Runout Protection Failure 323.9 53.1 1.4 ft2, 100.6% Power - FCV Failure 289.483 3.11 1.4 ft2, 100.6% Power - FWIV Failure 289.483 3.11 1.4 ft2, 100.6% Power - MSIV Failure 286.96 3.31 1.4 ft2, 0% Power - AFW Pump Runout Protection Failure 287.37 3.16 1.4 ft2, 0% Power - FCV Failure 287.30 3.21 1.4 ft2, 0% Power - FWIV Failure 287.28 3.21 1.4 ft2, 0% Power - MSIV Failure 288.28 2.51 Containment Functional Design 6.2.1-147 | |||
WATTS BAR WBNP-112 Table 6.2.1-44 Small Break Analysis - Small Split - Associated Times Maximum Lower 1 | |||
Case Compartment Time, Tmax (ft2) Temperature (°F) (sec) 0.86 325.34 83.28 0.944 325.12 80.46 0.6 325.1 112.9 0.35 324.4 191.4 0.1 317.74 646.77 1 All with AFW pump runout protection failure and 30% power, except that 0.86 ft2 break is at 100.6% | |||
power. | |||
6.2.1-148 Containment Functional Design | |||
WATTS BAR WBNP-112 Table 6.2.1-45 Safety Injection Flow Minimum Safeguards Injection Mode RCS Pressure (psia) Total Flow (gpm) 15.0 4,767.77 28.2 4,594.73 55.0 4,309.98 115.0 3,456.89 175.0 2,047.63 215.0 866.15 315.0 835.40 Injection Mode (Post-Reflood Phase) | |||
RCS Pressure (psia) Total Flow (gpm) 13.5 4,594.73 Cold Leg Recirculation Mode (w/o Residual Heat Removal [RHR] Spray) | |||
RCS Pressure (psia) Total Flow (gpm) 0 3,093 Cold Leg Recirculation Mode (w/ RHR Spray) | |||
RCS Pressure (psia) Total Flow (gpm) 0 794 Containment Functional Design 6.2.1-149 | |||
WATTS BAR WBNP-112 THIS PAGE INTENTIONALLY BLANK 6.2.1-150 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-1 Containment Pressure Versus Time Containment Functional Design 6.2.1-151 | |||
WATTS BAR 6.2.1-152 Containment Functional Design Figure 6.2.1-2a Upper Compartment Temperature Versus Time WBNP-112 | |||
WATTS BAR WBNP-112 Figure 6.2.1-2b Lower Compartment Temperature Versus Time Containment Functional Design 6.2.1-153 | |||
WATTS BAR WBNP-112 Figure 6.2.1-3 Active and Inactive Sump Temperature Transients 6.2.1-154 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-4 Melted Ice Mass Transient Containment Functional Design 6.2.1-155 | |||
WATTS BAR WBNP-112 Figure 6.2.1-4a Comparison of Containment Pressure Versus Ice Melt 6.2.1-156 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-5 Plan at Equipment Rooms Elevation Containment Functional Design 6.2.1-157 | |||
WATTS BAR WBNP-112 Figure 6.2.1-6 Containment Section View 6.2.1-158 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-7 Plan View at Ice Condenser Elevation Ice Condenser Compartments Containment Functional Design 6.2.1-159 | |||
WATTS BAR WBNP-112 Figure 6.2.1-8 Layout of Containment Shell Containment Functional Design 6.2.1-160 | |||
WATTS BAR WBNP-112 Figure 6.2.1-9 TMD Code Network Containment Functional Design 6.2.1-161 | |||
WATTS BAR WBNP-112 Figure 6.2.1-10 Upper and Lower Compartment Pressure Transient for Worst Case Break Compartment (Element 1) Having a DEHL Break 6.2.1-162 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-11 Upper and Lower Compartment Pressure Transient for Worst Case Break Compartment (Element 1) Having a DECL Break. | |||
Containment Functional Design 6.2.1-163 | |||
WATTS BAR WBNP-112 Figure 6.2.1-12 Illustration of Choked Flow Characteristics 6.2.1-164 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-13 Sensitivity of Peak Pressure to Air Compression Ratio Containment Functional Design 6.2.1-165 | |||
WATTS BAR WBNP-112 Figure 6.2.1-14 Steam Concentration in a Vertical Distribution Channel 6.2.1-166 Containment Functional Design | |||
WATTS BAR Containment Functional Design Figure 6.2.1-15 Peak Compression Pressure Versus Compression Ratio WBNP-112 6.2.1-167 | |||
WATTS BAR 6.2.1-168 Containment Functional Design WBNP-112 Figure 6.2.1-16 Peak Compartment Pressure versus Blowdown Rate | |||
WATTS BAR WBNP-112 Figure 6.2.1-17 Sensitivity of Peak Compression Pressure to Deck Bypass Containment Functional Design 6.2.1-169 | |||
WATTS BAR WBNP-112 Figure 6.2.1-18 Pressure Increase Versus Deck Area From Deck Leakage Tests 6.2.1-170 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-19 Energy Release at Time of Compression Peak Pressure From Full-Scale Section Tests with 1-Foot Diameter Baskets Containment Functional Design 6.2.1-171 | |||
WATTS BAR WBNP-112 Figure 6.2.1-20 Pressure Increase Versus Deck Area From Deck Leakage Tests 6.2.1-172 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-21 Deleted by Amendment 97 Containment Functional Design 6.2.1-173 | |||
WATTS BAR WBNP-112 Figure 6.2.1-22 Deleted by Amendment 97 6.2.1-174 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-23 Deleted by Amendment 97 Containment Functional Design 6.2.1-175 | |||
WATTS BAR WBNP-112 Figure 6.2.1-24 Deleted by Amendment 97 6.2.1-176 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-25 Deleted by Amendment 97 Containment Functional Design 6.2.1-177 | |||
WATTS BAR WBNP-112 Figure 6.2.1-26 Deleted by Amendment 97 6.2.1-178 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-27 Containment Model Schematic. | |||
Containment Functional Design 6.2.1-179 | |||
WATTS BAR WBNP-112 Figure 6.2.1-28 Reactor Cavity TMD Network. | |||
6.2.1-180 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-29 Reactor Vessel Annulus Containment Functional Design 6.2.1-181 | |||
WATTS BAR WBNP-112 Figure 6.2.1-30 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-182 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-31 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-183 | |||
WATTS BAR WBNP-112 Figure 6.2.1-32 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-184 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-33 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-185 | |||
WATTS BAR WBNP-112 Figure 6.2.1-34 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-186 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-35 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-187 | |||
WATTS BAR WBNP-112 Figure 6.2.1-36 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-188 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-37 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-189 | |||
WATTS BAR WBNP-112 Figure 6.2.1-38 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-190 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-39 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-191 | |||
WATTS BAR WBNP-112 Figure 6.2.1-40 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-192 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-41 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-193 | |||
WATTS BAR WBNP-112 Figure 6.2.1-42 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-194 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-43 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-195 | |||
WATTS BAR WBNP-112 Figure 6.2.1-44 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-196 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-45 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-197 | |||
WATTS BAR WBNP-112 Figure 6.2.1-46 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-198 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-47 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-199 | |||
WATTS BAR WBNP-112 Figure 6.2.1-48 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-200 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-49 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-201 | |||
WATTS BAR WBNP-112 Figure 6.2.1-50 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-202 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-51 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-203 | |||
WATTS BAR WBNP-112 Figure 6.2.1-52 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-204 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-53 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-205 | |||
WATTS BAR WBNP-112 Figure 6.2.1-54 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-206 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-55 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-207 | |||
WATTS BAR WBNP-112 Figure 6.2.1-56 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-208 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-57 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-209 | |||
WATTS BAR WBNP-112 Figure 6.2.1-58 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-210 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-59 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-211 | |||
WATTS BAR WBNP-112 Figure 6.2.1-60 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-212 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-61 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-213 | |||
WATTS BAR WBNP-112 Figure 6.2.1-62 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-214 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-63 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-215 | |||
WATTS BAR WBNP-112 Figure 6.2.1-64 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-216 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-65 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-217 | |||
WATTS BAR WBNP-112 Figure 6.2.1-66 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-218 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-67 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) | |||
Containment Functional Design 6.2.1-219 | |||
WATTS BAR WBNP-112 Figure 6.2.1-68 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-220 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-69 Compartment Temperature 1.4 ft2/Loop, 100.6% Power AFW Runout Protection Failure Containment Functional Design 6.2.1-221 | |||
WATTS BAR WBNP-112 Figure 6.2.1-70 Lower Compartment Pressure 1.4 ft2 Loop, 100.6% Power AFW Runout Protection Failure 6.2.1-222 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-71 Compartment Temperature 0.35 ft2 Split, 30% Power AFW Runout Protection Failure Containment Functional Design 6.2.1-223 | |||
WATTS BAR WBNP-112 Figure 6.2.1-72 Lower Compartment Pressure 0.35 ft2 Split, 30% Power AFW Runout Protection Failure 6.2.1-224 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-73 Compartment Temperature 0.6 ft2 Split, 30% Power AFW Runout Protection Failure Containment Functional Design 6.2.1-225 | |||
WATTS BAR WBNP-112 Figure 6.2.1-74 Lower Compartment Pressure 0.6 ft2 Split, 30% Power AFW Runout Protection Failure 6.2.1-226 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-75 Maximum Reverse Pressure Differential Model Containment Functional Design 6.2.1-227 | |||
6.2.1-228 WATTS BAR Figure 6.2.1-76 Maximum Reverse Pressure Differential Upper and Lower Compartment Pressures WBNP-112 Containment Functional Design | |||
WATTS BAR Containment Functional Design Figure 6.2.1-77 Maximum Reverse Pressure Differential Upper and Lower Compartment Temperatures WBNP-112 6.2.1-229 | |||
6.2.1-230 WATTS BAR Figure 6.2.1-78 Maximum Reverse Pressure Differential Upper to Lower Compartment Flowrates WBNP-112 Containment Functional Design | |||
WATTS BAR Containment Functional Design Figure 6.2.1-79 Maximum Reverse Pressure Differential Case 6 Upper and Lower Compartment Pressures WBNP-112 6.2.1-231 | |||
6.2.1-232 WATTS BAR Figure 6.2.1-80 Maximum Reverse Pressure Differential Case 6 Upper and Lower Compartment Temperatures WBNP-112 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-81 Steam Generator Enclosure Nodalization Containment Functional Design 6.2.1-233 | |||
6.2.1-234 WATTS BAR Figure 6.2.1-82 Flow Paths For TMD Steam Generator Enclosure Short-term Pressure Analysis WBNP-112 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-83 Pressure Transient Between Break Element And Upper Compartment (Steam Generator Enclosure Analysis) | |||
Containment Functional Design 6.2.1-235 | |||
WATTS BAR WBNP-112 Figure 6.2.1-84 Differential Pressure Transient Across The Steam Generator Vessel (Steam Generator Enclosure Analysis) 6.2.1-236 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-85 Differential Pressure Transient Across The Steam Generator Vessel (Steam Generator Enclosure Analysis) | |||
Containment Functional Design 6.2.1-237 | |||
WATTS BAR WBNP-112 Figure 6.2.1-86 Pressure Versus Time For The Break Element (Steam Generator Enclosure Analysis) 6.2.1-238 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-86a Upper Compartment Pressure Versus Time (Steam Generator Enclosure Analysis) | |||
Containment Functional Design 6.2.1-239 | |||
WATTS BAR WBNP-112 Figure 6.2.1-87 Nodalization Pressure Enclosure Analysis 6.2.1-240 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-88 Pressure Transient Between Break Element And Upper Compartment (Pressurizer Enclosure Analysis) | |||
Containment Functional Design 6.2.1-241 | |||
WATTS BAR WBNP-112 Figure 6.2.1-89 Pressure Differential Across The Pressurizer Vessel (Pressurizer Enclosure Analysis) 6.2.1-242 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-90 Pressure Differential Across The Pressurizer Vessel (Pressurizer Enclosure Analysis) | |||
Containment Functional Design 6.2.1-243 | |||
WATTS BAR WBNP-112 Figure 6.2.1-91 Pressure Differential Across The Pressurizer Vessel (Pressurizer Enclosure Analysis) 6.2.1-244 Containment Functional Design | |||
WATTS BAR WBNP-112 Figure 6.2.1-92 Pressure Versus Time For The Break Element (Pressurizer Enclosure Analysis) | |||
Containment Functional Design 6.2.1-245 | |||
Containment Functional Design 6.2.1- | |||
WATTS BAR WBNP-112 THIS PAGE INTENTIONALLY BLANK 6.2.1-246 Containment Functional Design | |||
WATTS BAR WBNP-112 6.2.2 CONTAINMENT HEAT REMOVAL SYSTEMS Adequate containment heat removal capability for the ice condenser reactor containment is provided by the ice condenser (Section 6.7), the air return fan system (Section 6.8), and two separate containment heat removal spray systems whose components operate in the sequential modes described in Section 6.2.2.2. One of these heat removal spray systems is the containment spray system, and the second is the residual heat removal spray system, which is a portion of the residual heat removal system (Section 6.3). | |||
Minimum engineered safety feature performance of the containment heat removal systems is achieved with the following: | |||
(1) Ice condenser (Section 6.7) | |||
(2) One train of the air return fan system (3) One train of the containment spray system (4) One train of the residual heat removal spray system (not required for steam or feed line break) | |||
Each spray system consists of two trains of redundant equipment per reactor unit. | |||
There are four spray headers per unit. Two headers are supplied from separate trains of the containment spray system; the other two are supplied by separate trains of the RHR spray system. Each individual train consists of a pump, a heat exchanger, appropriate control valves, required piping, and a header with nozzles located in the upper compartment of the containment with flow directed to obtain full coverage of the containment upper volume during an emergency. The systems use borated water supplied from the refueling water storage tank and/or the recirculation sump. | |||
6.2.2.1 Design Bases The primary design basis for the containment heat removal spray systems is to spray cool water into the containment atmosphere when appropriate in the event of a loss-of-coolant accident or secondary side break and thereby ensure that the containment pressure cannot exceed the containment shell maximum internal pressure of 15.0 psig at 250°F, which corresponds to the code design internal pressure of 13.5 psig at 250°F (see Section 3.8.2). This protection is afforded for all pipe break sizes up to and including the hypothetical instantaneous circumferential rupture of the reactor coolant loop resulting in unobstructed flow from both pipe ends. After the ice has melted, the containment spray system and the residual heat removal spray system become the sole systems for removing energy directly from the containment. The containment heat removal systems are designed to provide a means of removing containment heat without loss of functional performance in the post-accident containment environment and operate without benefit of maintenance for the duration of time to restore and maintain containment conditions at atmospheric pressure. Although the water in the core after a loss-of-coolant accident is quickly subcooled by the emergency core cooling system (Section 6.3), the design of heat removal capability of each CONTAINMENT HEAT REMOVAL SYSTEMS 6.2.2-1 | |||
WATTS BAR WBNP-112 containment heat removal system is based on the conservative assumption that the core residual heat is released to the containment as steam which eventually melts all ice in the ice condenser. | |||
The containment spray system provides two redundant heat removal trains. The system is designed such that both trains are automatically started by high-high containment pressure signal. The signal actuates, as required, all controls for positioning all valves to their operating position and starts the pumps. The operator can also manually actuate the entire system from the control room. Either of the two trains containing a pump, heat exchanger, and associated valving and spray headers is independently capable of delivering a minimum flowrate of 4,000 gpm. | |||
The containment heat removal spray systems are designed to withstand the design basis earthquake and the operational basis earthquake without loss of function. They satisfy the TVA Class B Mechanical Requirements. The heat exchanger tube side (CSS) meets TVA Class B and the shell side (ERCW) meets TVA Class C mechanical requirements. The containment heat removal spray systems maintain their integrity and do not suffer loss of ability to perform their minimum required function due to normal operation, faults of moderate frequency, infrequent faults, and limiting faults. | |||
Sufficient redundancy for all supporting systems necessary for minimum operational requirements of the containment heat removal spray systems is provided and complies with the single failure criteria for engineered safety features. Separate divisions on essential raw cooling water supply, power equipment heat exchangers, pumps, valves, and instrumentation are provided in order to have two completely separated trains. | |||
The system is provided with overpressure protection from excessive pressures that could otherwise result from temperature changes, interconnection with other systems operating at higher pressures, or other means. | |||
Those portions of the containment heat removal spray systems located outside of the containment which are designed to circulate, during post-accident conditions, radioactively contaminated water collected in the containment meet the following requirements: | |||
(1) Shielding within guidelines of 10 CFR 20 and 10 CFR 100. | |||
(2) Collection of discharges from pressure relieving devices. | |||
(3) Remote means for isolating any sections under anticipated malfunction or failure conditions. | |||
(4) Means to detect and control radioactivity leakage into the environs to limits consistent with guidelines set forth in 10 CFR 20 and 10 CFR 100. | |||
During accident conditions, cooling of the containment spaces is provided by the ice condenser system, containment heat removal spray systems, and the air return system. In addition, during non-LOCA accidents, the lower compartment cooler (LCC) fans are utilized to recirculate air throughout the lower containment spaces to prevent 6.2.2-2 CONTAINMENT HEAT REMOVAL SYSTEMS | |||
WATTS BAR WBNP-112 hot pockets from developing. The LCC units may be operated continuously throughout all accidents, except a MSLB, which do not initiate a containment Phase B isolation signal. After a MSLB all four coolers (2 Train A and 2 Train B) are started although only 2 are required, within 11/2 hours to 4 hours after the MSLB to recirculate air throughout the lower containment spaces, to prevent hot spots from developing. During or after a LOCA, the LCC units, including their fans, are not required to be operable. | |||
6.2.2.2 System Design The containment spray systems consist of two separate trains of equal capacity with each train independently capable of meeting system requirements. This system can be supplemented with two residual heat removal system pumps and two residual heat exchangers in parallel, with associated piping, valves and individual spray headers in the upper containment volume. Each train includes a pump, heat exchanger, ring header with nozzles, isolation valves and associated piping, and instrumentation and controls. Partial flow from an RHR system pump through its associated heat exchanger can be used to supplement each train. Independent electrical power supplies are provided for equipment in each containment spray train. In addition each train is provided with electrical power from separate emergency diesel generators in the event of a loss of offsite electrical power. During normal operation, all of the equipment is idle and the associated isolation valves are closed. | |||
Upon system activation during a LOCA or other high energy line break, adequate containment cooling is provided by the containment spray systems whose components operate in sequential modes. These modes are: 1) spraying a portion of the contents of the refueling water storage tank into the containment atmosphere using the containment spray pumps; 2) after the refueling water storage tank has been drained, but while there is still ice remaining in the ice condenser, recirculation of water from the containment sump through the containment spray pumps, through the containment spray heat exchangers, and back to the containment (This spray is useful in reducing sump water temperatures.); 3) diversion of a portion of the recirculation flow from the residual heat removal system to additional spray headers. RHR spray operation is initiated manually by the operator only if the emergency core cooling system and containment spray system are both operating in the recirculation mode. If switchover to recirculation occurs prior to 1 hour after initiation of the LOCA, RHR spray operation can be commenced 1 hour after initiation of the LOCA. If switchover to recirculation occurs later than 1 hour after initiation of the LOCA, RHR spray operation can be commenced after completion of the switchover procedure. | |||
The spray water from the containment and RHR spray systems returns from the upper compartment to the lower compartment through two 14 inch drains in the bottom of the refueling canal. The curbing around the personnel access door and the equipment access hatch on the operating deck directs spray water flow towards the refueling canal. The air-water mixture entering the air return fans will be rerouted inside the polar crane wall through the accumulator rooms utilizing curbing, the floor hatch cover and floor drainage system. | |||
The flow diagram for this system is presented in Figure 6.2.2-1. | |||
CONTAINMENT HEAT REMOVAL SYSTEMS 6.2.2-3 | |||
WATTS BAR WBNP-112 Component Description Pumps The containment spray system flow is provided by two centrifugal type pumps driven by electric motors. The motors, which can be powered either normally or from an emergency source are direct coupled and non-overloading to the end of the pump curve. The design head of the containment spray pump is sufficient to ensure rated capacity with a minimum level in the refueling water storage tank or the containment sump when pumping against a head equivalent to the sum of the maximum pressure of the containment post LOCA/HELB, the elevational head between the pump discharge and the uppermost spray nozzles, and the equipment and piping friction losses. Each pump is rated for 4000 gpm flow at a design head of 435 ft. See Table 6.2.2-1 for additional design parameters and Figure 6.2.2-2 for characteristic curves. | |||
The residual heat removal pumps which also provide flow to the containment heat removal spray system are described in Section 5.5.7.2.1 and Table 5.5-8. | |||
Each residual heat removal pump provides a design flow of 2000 (1475 gpm analytical) for upper containment spray. | |||
Each containment spray pump is powered by a horizontal squirrel cage induction motor. Pump motor parameters are presented in Table 6.2.2-1. | |||
Net Positive Suction Head (NPSH) | |||
The plant and piping layout of the containment spray system ensures that the pump NPSH requirements are met at maximum runout conditions with the containment spray pumps taking suction from either the refueling water storage tank or the containment sump. The NPSH available from the containment sump is calculated using the maximum credible sump water temperature (190°F) with no credit taken for containment overpressure or height of water above the RHR Strainer Assembly. | |||
Available NPSH parameters are given in Table 6.3-12. | |||
Heat Exchangers The containment spray heat exchangers are the vertical counter flow U-tube type with tubes welded to the tube sheet. Borated water from either the refueling water storage tank or the containment sump circulates through the tube side. Design parameters are presented in Table 6.2.2-2. | |||
Piping All containment heat removal spray system piping in contact with borated water is austenitic stainless steel. All piping joints are welded except for the flanged connection at the pump or where disassembly of the joint may be required. | |||
Spray Nozzles and Ring Headers Each containment spray ring header provides 4000 gpm minimum and contains 263 hollow cone ramp bottom nozzles, each of which is capable of a design flow of 15.2 6.2.2-4 CONTAINMENT HEAT REMOVAL SYSTEMS | |||
WATTS BAR WBNP-112 gpm with a 40 psi differential pressure. These nozzles have an approximately 3/8-inch diameter spray orifice and are not subject to clogging by particles less than 1/4 inch in maximum dimension. The nozzles produce a drop size spectrum with a median diameter of less than 700 microns at 40 psid. The spray solution is completely stable and soluble at all temperatures of interest in the containment and, therefore, does not precipitate or otherwise interfere with nozzle performance. Each nozzle header is independently oriented to maximize coverage of the containment volume inside the crane wall. This arrangement prohibits any flow into the ice condenser. | |||
The residual heat removal spray ring headers contain 146 nozzles per header and deliver a design flow of 2000 gpm (1475 gpm analytical) per header. Each RHR spray header will perform its required design function with 142 unobstructed spray nozzles. | |||
They have the same design characteristics as the headers in the containment spray system. | |||
Refueling Water Storage Tank During the injection phase immediately following a LOCA or HELB, the containment spray is supplied from the refueling water storage tank. | |||
Recirculation Sump The recirculation sump is described in Section 6.3.2.2 under the discussion of the recirculation mode. | |||
Material Compatibility All parts of the containment spray system in contact with borated water are austenitic stainless steel or equivalent corrosion resistant material. | |||
6.2.2.3 Design Evaluation Performance of the containment heat removal system is evaluated through analyses of the design basis accident and various other cases described in Chapter 15 and Section 6.2.1. The analyses were performed using the LOTIC code and show that the containment heat removal systems are capable of keeping the containment pressure below the containment maximum internal pressure of 15 psig, which corresponds to the code design internal pressure of 13.5 psig at 250°F (see Section 3.8.2) even when it is assumed that the minimum engineered safety features are operating. Section 6.2.1 presents a description of the analytical methods and models which were used along with verification of pertinent items from Waltz Mill tests, and curves showing the calculated performance of important variables following the design-basis loss-of-coolant accident. | |||
The design basis accident analysis (Section 6.2.1.3.3) results in a required containment spray flow rate of 4000 gpm using 88°F** constant temperature essential raw cooling water for the heat exchangers. | |||
1 **Note: The containment analysis was run at ERCW temperature of 88°F although the containment spray, component cooling, and residual heat removal Hx UA values are based on ERCW temperature of 85°F to provide additional conservatism. | |||
CONTAINMENT HEAT REMOVAL SYSTEMS 6.2.2-5 | |||
WATTS BAR WBNP-112 The containment spray systems provide two full-capacity heat removal systems for the containment, each of which is sized as described in Section 6.2.2.1 to remove heat at a rate which precludes an increase of the containment maximum internal pressure above 15.0 psig, which corresponds to the code design internal pressure of 13.5 psig at 250°F (see Section 3.8.2). All spray headers and spray nozzles are located inside the containment in the upper compartment and can withstand, without loss of function or maintenance, the post-accident containment environment. The remainder of the systems, with the exception of the refueling water storage tanks, which includes all active components, are located in the Auxiliary Building and, therefore, are not affected by wind, tornado, or snow and ice conditions. | |||
The design is based on the spray water being raised to the saturation temperature of the containment in falling through the steam-air mixture within the building. The minimum fall path of the droplets is approximately 75 ft from the spray ring headers to the operating deck. The actual fall path is longer due to the trajectory of the droplets sprayed out from the ring header nozzles. Figures 6.2.2-3 through 6.2.2-6 depict the containment spray coverage for the containment spray system. | |||
Except for the refueling water storage tank water supplied by the safety injection system, the containment spray system initially operates independently of other engineered safety features. For extended operation in the recirculation mode, water is supplied to the containment RHR spray headers through the residual heat removal pumps and residual heat removal exchangers. One containment spray system train, supplemented by one RHR spray train, when required, provides adequate heat removal capability to limit containment pressure below design (see Section 6.2.1.3). | |||
RHR spray is required only after switchover to the recirculation mode and no earlier than 1 hour after initiation of the LOCA. At this time one RHR pump can provide sufficient RHR spray as well as adequate core flow via the high head (one centrifugal charging and one safety injection) pumps. (See Section 6.3.3 for the performance evaluation of the RHR pumps in their core cooling function.) | |||
All active components of the system were analyzed to show that the failure of any single active component does not prevent fulfilling the design function. This analysis is summarized in Table 6.2.2-3. A single failure in the residual heat removal system will not prevent long-term use of the spray system. The analyses of the loss-of-coolant accident presented in Chapter 15 reflect the single failure analysis. Each of the spray trains provides complete backup for the other. | |||
An analysis of the spray return drains located in the refueling canal has been made to show that they are adequately sized for a maximum RHR and containment spray flow and ensures an adequate water supply in the lower compartment to satisfy pump NPSH requirements. | |||
The passive portions of the spray systems located within the containment are designed to withstand, without loss of functional performance, a post accident containment environment and to operate without benefit of maintenance. | |||
6.2.2-6 CONTAINMENT HEAT REMOVAL SYSTEMS | |||
WATTS BAR WBNP-112 The spray headers which are located in the upper containment volume are separated from the reactor and primary coolant loops by the operating deck and inner wall of the ice bed. These spray headers are therefore protected from missiles originating in the lower compartment. | |||
This evaluation shows that the containment spray systems can withstand expected conditions during the 40-year life of the plant without loss of capability to perform the required safety functions. Specifically, the system achieved this by having been designed to meet applicable General Design Criteria (GDC) as follows: | |||
(1) The systems can withstand the effects of natural phenomena as required by GDC 2. | |||
(2) The systems are designed to accommodate the effects of and be compatible with the environmental conditions associated with normal operation, maintenance, testing, and postulated accidents including loss of coolant as required by GDC 4. | |||
(3) The systems are not shared with another nuclear power unit as required by GDC 5. | |||
(4) The systems are designed to be capable of being inspected and tested to ensure reliability throughout their life as required by GDC 39 and 40. | |||
(5) The systems are designed adequately to provide post-accident cooling inside the primary containment to reduce the containment pressure and temperature following any LOCA and maintain them at acceptable levels, as required by GDC 38. | |||
(6) The systems are designed to aid in the control and removal of fission products, hydrogen, oxygen, and other substances which may be released into the reactor containment following postulated accidents to assure that containment integrity is maintained, as required by GDC 41. | |||
Tritium Production Core Evaluation (Unit 1 Only) | |||
The effects of converting WBN to a Tritium Production Core (TPC) on the containment heat removal systems have been evaluated. The evaluation includes the effect of adding a leading edge flow meter (LEFM) into the main feedwater piping and the effect of uprating the plant nominal power level by 1.4%. | |||
Based on the conclusions in Section 6.2.3.12 that mass and energy releases for LOCA and secondary side pipe ruptures do not have an adverse impact on the primary containment functionality due to incorporation of a TPC, the containment heat removal system will not be impacted. | |||
6.2.2.4 Testing and Inspections Performance tests of the active components in the system are performed in the manufacturer's plant and followed by in-place preoperational testing. | |||
CONTAINMENT HEAT REMOVAL SYSTEMS 6.2.2-7 | |||
WATTS BAR WBNP-112 Capability is provided to test initially and subsequently on a routine basis to the extent practical the operational startup sequence and performance capability of the containment spray system including the transfer to alternate power sources. | |||
Capability to test periodically the delivery capacity of the containment spray system at a position as close to the spray header as is practical and for obstruction of the spray nozzles is provided. As part of the preoperational test program, the containment spray nozzles are physically verified to pass an unobstructed flow of air. The air is introduced into the headers through an air test connection on each header. | |||
Initially, the containment spray system is hydrostatically tested to the applicable code test pressure. | |||
All periodic tests of individual components or the complete containment spray system are controlled to ensure that plant safety is not jeopardized and that undesirable transients do not occur. | |||
The containment spray system is designed to comply with ASME Section XI, "Inservice Inspection of Nuclear Reactor Coolant System." Detailed test procedures are given in Chapter 14. | |||
6.2.2.5 Instrumentation Requirements The containment spray system is actuated either manually from the control room or external to the main control room or automatically by the coincidence of two sets out of four protection set loops monitoring the lower containment pressure. The high-high containment pressure signal starts the containment spray pumps and positions all valves to their operating configuration. | |||
The operation of the containment spray system is verified by instrument readout in the control room. Pump motor breakers energize indicating lights on the control panel to show power is being supplied to the pump motors. Status lights on the main control panel indicate valve position and are energized independently of the valve actuation signal. | |||
To protect the pumps from low flow conditions, a mini-flow recirculation line is provided to allow pump discharge to be circulated back into the pump suction line. This line is opened by a motor-operated valve when flow in the discharge line drops below that required for pump protection or if, upon starting, flow is not achieved in the spray header within a preset time interval. Elbow taps in each discharge line provide a delta-p measurement to monitor the flow rate and provide the flow signal for the control room flow indicators and to control the minimum flow recirculation valve. | |||
Local instruments monitor the following parameters: containment spray pump suction and discharge pressure, heat exchanger inlet temperature, heat exchanger inlet and outlet pressure, and containment spray test line flow. | |||
In the event of a main control room evacuation, the necessary control functions are transferable to outside of the main control room in order to assure that the system can be aligned and locked to prevent inadvertent operation and to manually initiate system 6.2.2-8 CONTAINMENT HEAT REMOVAL SYSTEMS | |||
WATTS BAR WBNP-112 operation if necessary. The control transfer is provided for the spray pumps, containment spray isolation valves, and containment sump isolation valves. | |||
The system is designed as Seismic Category I. The instrumentation and associated interconnected wiring and cables are physically and otherwise separated so that a single event cannot cause malfunction of the entire system. | |||
6.2.2.6 Materials All parts of the containment spray system in contact with borated water are austenitic stainless steel or equivalent corrosion-resistant material. None of these materials produce radiolytic or pyrolytic decomposition products that can interfere with this or other engineered safety features. | |||
CONTAINMENT HEAT REMOVAL SYSTEMS 6.2.2-9 | |||
6.2. | |||
WATTS BAR WBNP-112 Table 6.2.2-1 Containment Spray Pump/Motor Design Parameters Pump Quantity Per Unit 2 Design Pressure, psig 300 Design Temperature, °F 250 Design Flow Rate, gpm 4000 Design Head, ft 435 Motor Horsepower, hp 700 Service Factor 1.15 Voltage, V 6600 Phase 3 Cycles, Hz 60 6.2.2-10 CONTAINMENT HEAT REMOVAL SYSTEMS | |||
WATTS BAR WBNP-112 Table 6.2.2-2 Containment Spray Heat Exchanger Design Parameters Quantity Per Unit 2 Type Counter Flow Percent Tubes Plugged 10% | |||
Heat Transfer Per Unit, Btu/hr 12.85 x 107 Shell-Side Flow, gpm 5,200 Tube-Side Flow, gpm 4,000 Tube-Side Inlet Temperature, °F 190 Shell-Side Inlet Temperature, °F 85 Tube-Side Outlet Temperature, °F 124.7 Shell-Side Outlet Temperature, °F 129.5 Design Pressure (Shell/Tube), psig 150/300 Design Temperature (Shell/Tube), °F 200/250 Heat Exchanger UA, Btu/hr-°F 2.44 x 106 CONTAINMENT HEAT REMOVAL SYSTEMS 6.2.2-11 | |||
& | |||
6.2 | 6.2.2-12 Table 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS (Page 1 of 8) | ||
ITEM FAILURE POTENTIAL METHOD OF EFFECTS ON EFFECT ON NO.COMPONENT FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS WATTS BAR INJECTION MODE | |||
: 1. Containment To pump borated Fails to start Mechanical Indication via CS System None. Two Only one train is Spray Pump A-A water to spray failure or switches HS-72-27A Train "A" is lost 100% capacity required to nozzles in the electrical & -27C trains are mitigate accident containment failure due to provided. consequences. | |||
Containment | loss of power | ||
: 2. Containment Spray To pump borated Fails to start Mechanical Indication via CS System None. Two Only one train is Pump B-B water to spray failure or switches HS-72-10A Train "B" is lost 100% capacity required to nozzles in the electrical & -10C trains are mitigate accident containment failure due to provided. consequences. | |||
loss of power | |||
: 3. Valve FCV 72-21 Provide water flow Fails closed Mechanical Valve position CS System None. CS Only one train is path to CS PMP B-B failure indication via switch Train "B" is System Train required to blockage or HS-72-21A inoperable "A" is used to mitigate accident spurious supply water consequences. | |||
electrical signal to nozzles | |||
: 4. Valve FCV 72-22 Provide water flow Fails Closed Mechanical Valve position CS System None. CS Only one train is path to CS PMP A-A failure indication via switch Train "A" is System train required to blockage or HS-72-22A inoperable "B" is used to mitigate accident spurious supply water consequences. | |||
electrical signal to nozzles CONTAINMENT HEAT REMOVAL SYSTEMS WBNP-112 | |||
6.2.2- | Table 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS (Page 2 of 8) | ||
ITEM FAILURE POTENTIAL METHOD OF EFFECTS ON EFFECT ON NO.COMPONENT FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS WATTS BAR | |||
: 5. Valve FCV 72-02 Water flow path to Fails to open Mechanical Valve position CS System None. Two Only one train is containment spray failure or loss indication via Train "B" is lost 100% capacity required to nozzles of power to switches trains are mitigate accident valve motor HS-72-2A/ provided. consequences. | |||
HS-72-2B* | |||
Recloses Mechanical Valve position CS System None. Two Only one train is CONTAINMENT HEAT REMOVAL SYSTEMS after opening failure or indication via Train "B" is lost 100% capacity required to spurious switches trains are mitigate accident electrical signal HS-72-2A/HS-72-2B provided. consequences. | |||
: 6. Valve FCV 72-039 Water flow path to Fails to open Mechanical Valve position CS System None. Two Only one train is containment spray failure or loss indication via Train "A" is lost 100% capacity required to nozzles of power to switches trains are mitigate accident valve motor HS-72-39A/ provided. consequences. | |||
HS-72-39B Recloses Mechanical Valve position CS System None. Two Only one train is after opening failure or indication via Train "A" is lost 100% capacity required to spurious switches trains are mitigate accident electrical signal HS-72-39A/ provided. consequences. | |||
HS-72-39B | |||
: 7. Emergency power Provide power to Fails Diesel Voltmeters in CS System None. Two Only one train is to Train A PMP A motor & all generator Control Room Train "A" is lost 100% capacity required to MOVs in Train A shutdown Bd. trains are mitigate accident 1A-A failure provided. consequences. | |||
* Note: Valve position indication for Valve FCV-72-02 may be derived from indicator lights on all three hand switches (HS-72-2A, HS-72-2B or HS-72-2C). This is unique in that 2B hand switches have been removed from nearly all other applied uses due to EQ considerations. | |||
6.2.2-13 WBNP-112 | |||
6.2.2- | |||
failure | Table 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS 6.2.2-14 (Page 3 of 8) | ||
ITEM FAILURE POTENTIAL METHOD OF EFFECTS ON EFFECT ON NO.COMPONENT FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS WATTS BAR | |||
: 8. Emergency Power Provide power to Fails Diesel Voltmeters in CS System None. Two Only one train is to Train B PMP B motor & all generator Control Room Train "B" is lost 100% capacity required to MOVs in Train B shutdown Bd. trains are mitigate accident 1B-B failure provided. consequences. | |||
: 9. FCV-72-34 Isolate pump A-A Fails open Mechanical Valve position Water flowing Train "A" Only one train is discharge from failure or indication via switch into spray capability required to suction spurious HS-72-34A nozzles will be reduced. No mitigate accident electrical signal diminished. impact on consequences. | |||
plant; operator can put 100% | |||
train B in operation. | |||
: 10. FCV-72-13 Isolate pump B-B Fails open Mechanical Valve position Water flowing Train "B" Only one train is discharge from failure or indication via switch into spray capability required to suction spurious HS-72-13A nozzles will be reduced. No mitigate accident electrical signal reduced. impact on consequences. | |||
plant; operator can put 100% | |||
train A in operation. | |||
: 11. Check VA.72-506 Flow path to CS Valve stuck Mechanical Pump discharge Train A is None. Two Pump A-A closed failure flow indicator inoperable 100% | |||
FI-72-34 capability trains are provided. | |||
CONTAINMENT HEAT REMOVAL SYSTEMS WBNP-112 | |||
Table 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS (Page 4 of 8) | |||
ITEM FAILURE POTENTIAL METHOD OF EFFECTS ON EFFECT ON NO.COMPONENT FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS WATTS BAR | |||
: 12. Check VA 72-507 Flow path to CS Valve stuck Mechanical Pump discharge Train B is None. Two Pump B-B closed failure flow indicator inoperable 100% | |||
FI-72-13 capability trains are provided. | |||
: 13. Check VA 72-524 CS Pump A-A Valve stuck Mechanical Flow measurement Train A is None. Two CONTAINMENT HEAT REMOVAL SYSTEMS discharge flow path closed failure via flow indicator inoperable 100% | |||
FI-72-34 capability trains are provided. | |||
: 14. Check VA 72-525 CS Pump B-B Valve stuck Mechanical Flow measurement Train B is None. Two discharge flow path closed failure via flow indicator inoperable 100% | |||
FI-72-13 capability trains are provided. | |||
: 15. Check VA 72-548 Flow path to Train A Valve stuck Mechanical Pump discharge via Train A is None. Two spray nozzles closed failure flow indicator inoperable 100% | |||
FI-72-34 capability trains are provided. | |||
: 16. Check VA 72-549 Flow path to Train B Valve stuck Mechanical Pump discharge via Train B is None. Two spray nozzles closed failure flow indicator inoperable 100% | |||
FI-72-13 capability trains are provided. | |||
6.2.2-15 WBNP-112 | |||
failure | Table 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS 6.2.2-16 (Page 5 of 8) | ||
ITEM FAILURE POTENTIAL METHOD OF EFFECTS ON EFFECT ON NO.COMPONENT FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS WATTS BAR | |||
: 17. Relief VA 72-508 CS Pump A-A Valve fails Mechanical Train A capacity None. Two suction piping over- open failure will be 100% capacity pressure protection diminished trains provided. | |||
: 18. Relief VA 72-509 CS Pump B-B Valve fails Mechanical Train B capacity None. Two suction piping over- open failure will be 100% capacity pressure protection diminished trains provided. | |||
RECIRC. MODE ACTIVE FAILURE | |||
: 19. Valve FCV-72-44 Train A flow path Fails to open Mechanical Valve position Train "A" is None. Two from containment or recloses failure or indication via inoperable 100% capacity sump after opening electrical switches trains are failure HS-72-44A, provided. | |||
HS-72-44B, HS-72-44C 20 Valve FCV-72-45 Train B flow path Fails to open Mechanical Valve position Train "B" is None. Two from containment or recloses failure or indication via inoperable 100% capacity sump after opening electrical switches trains are failure HS-72-45A, provided. | |||
HS-72-45B, HS-72-45C CONTAINMENT HEAT REMOVAL SYSTEMS WBNP-112 | |||
Table 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS (Page 6 of 8) | |||
ITEM FAILURE POTENTIAL METHOD OF EFFECTS ON EFFECT ON NO.COMPONENT FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS WATTS BAR | |||
: 21. Valve FCV-72-22 Isolate "RWST" Fails to close Mechanical Valve position Train "A" is None. Two Interlock will during recirc. mode failure or indication via switch inoperable 100% capacity prevent opening electrical HS-72-22A trains are of FCV-72-44. | |||
failure provided. | |||
: 22. Valve FCV-72-21 Isolate "RWST" Fails to close Mechanical Valve position Train "B" is None. Two Interlock will CONTAINMENT HEAT REMOVAL SYSTEMS during recirc. mode failure or indication via switch inoperable 100% capacity prevent opening electrical HS-72-21A trains are of FCV-72-45. | |||
failure provided. | |||
: 23. Containment Cools containment ERCW flow ERCW Train A High CS water CS water in None. 100% | |||
Spray Heat spray water lost system temp. indication via Train A can not capacity Train Exch. A mechanical or ICS point T0168A be cooled. B will be electrical operated. | |||
failure | |||
: 24. Containment Cools containment ERCW flow ERCW Train B High CS water CS water in None. 100% | |||
Spray Heat spray water lost system temp. indication via Train B can not capacity Train Exch. B mechanical or ICS point T0169A. be cooled. A will be electrical operated. | |||
failure | |||
: 25. Check VA 72-506 Isolate RWST Valve stuck Mechanical None. Valve None. | |||
during recirc. mode open failure FCV-72-22 will isolate RWST. | |||
: 26. Check VA 72-507 Isolate RWST Valve stuck Mechanical None. Valve None. | |||
during recirc. mode open failure FCV-72-21 will isolate RWST. | |||
6.2.2-17 WBNP-112 | |||
Table 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS 6.2.2-18 (Page 7 of 8) | |||
ITEM FAILURE POTENTIAL METHOD OF EFFECTS ON EFFECT ON NO.COMPONENT FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS WATTS BAR PASSIVE | |||
: 27. Containment Cools CS water Clogging/ Impurities, High CS water Diminished heat None. Two Only one train is Spray Heat during recirc. mode tube rupture particulate Temp. indication via transfer 100% capacity required to Exch. A matter ICS point T0168A capability in trains mitigate accident Train A including heat consequences. | |||
exchangers are provided. | |||
: 28. Containment Cools CS water Clogging/ Impurities, High CS water Diminished heat None. Two Only one train is Spray Heat during recirc. mode tube rupture particulate Temp. indication via transfer 100% capacity required to Exch. B matter ICS point T0169A. capability in trains mitigate accident Train B including heat consequences. | |||
exchangers are provided. | |||
: 29. Spray nozzles Spray water in the Clogged Impurities, Reduced pump flow 263 nozzles Redundant Nozzles are 3/8 containment particulate provided per trains are inch diameter matter. CSS train. Will provided to and Containment diminish cooling fulfill minimum Sump strainer capacity slightly. plant perforation size requirements. is 0.085 inch, so possibility of clogging is remote. | |||
: 30. Piping or valve Ruptures or In service Inspection System None. Two Only one train is body or pump major capability 100% capacity required to casing or HX, leakage diminished. trains are mitigate accident shell provided. consequences. | |||
CONTAINMENT HEAT REMOVAL SYSTEMS WBNP-112 | |||
Table 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS (Page 8 of 8) | |||
ITEM FAILURE POTENTIAL METHOD OF EFFECTS ON EFFECT ON NO.COMPONENT FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS WATTS BAR | |||
: 31. All valves Disc Mechanical System None. Two required for separated failure capability 100% capacity system operation from stem diminished trains are provided. | |||
CONTAINMENT HEAT REMOVAL SYSTEMS 6.2.2-19 WBNP-112 | |||
WATTS BAR WBNP-112 THIS PAGE INTENTIONALLY LEFT BLANK 6.2.2-20 CONTAINMENT HEAT REMOVAL SYSTEMS | |||
WATTS BAR Containment Heat Removal Systems Figure 6.2.2-1 Powerhouse Units 1 & 2 Mechanical Flow Diagram Containment Spray System WBNP-112 6.2.2-21 | |||
WATTS BAR WBNP-112 Figure 6.2.2-2 Containment Spray Pump Performance Curves Containment Heat Removal Systems 6.2.2-22 | |||
WATTS BAR Containment Heat Removal Systems Figure 6.2.2-3 Reactor Bldgs. Units 1 & 2 Mechanical Containment Spray System 6.2.2-23 Piping Plan of Spray Patterns From C.S. Loop Header A WBNP-112 | |||
[Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.2-4 Powerhouse-Auxiliary & Reactor Bldgs Units 1 & 2 Mechanical Containment Spray System Piping Containment Heat Removal Systems 6.2.2-24 | |||
WATTS BAR Containment Heat Removal Systems Figure 6.2.2-5 Reactor Bldgs. Units 1 & 2 Mechanical Containment Spray System Piping 6.2.2-25 Plan of Spray Patterns From C.S. Loop Header B WBNP-112 | |||
WATTS BAR Containment Heat Removal Systems Figure 6.2.2-6 Reactor Bldgs. Units 1 & 2 Mechanical Containment Spray System Piping Section of Spray Patterns From C.S. Loop Header B WBNP-112 6.2.2-26 | |||
WATTS BAR WBNP-112 6.2.3 Secondary Containment Functional Design Structures included as part of the secondary containment system are the Shield Building of each reactor unit, the Auxiliary Building, the Condensate Demineralizer Waste Evaporator (CDWE) Building and the essential raw cooling water (ERCW) pipe tunnels adjacent to the Auxiliary Building. Depending on the configuration of the plant, the Primary Containment Building(s) may also be included as a structure which is part of the secondary containment system. This condition exists when the primary containment is open to the Auxiliary Building. The emergency gas treatment system (EGTS) is provided for ventilation control and cleanup of the atmosphere inside the annulus between the Shield Building and the Primary Containment Building. The Reactor Building purge air system is also available for cleaning up the atmosphere inside the Shield Building Annulus. Refer to Section 9.4.6 for further details relating to the purge air system. The Auxiliary Building Gas Treatment System (ABGTS) provides a similar contamination control capability in the Auxiliary Building Secondary Containment Enclosure (ABSCE),which includes all of the areas listed above. | |||
6.2.3.1 Design Bases 6.2.3.1.1 Secondary Containment Enclosures Design bases for the secondary containment structures were devised to assure that an effective barrier exists for airborne fission products that may leak from the primary containment, or the Auxiliary Building fuel handling area, during a loss-of-coolant accident (LOCA). Within the scope of these design bases are requirements that influence the size, structural integrity, and leak tightness of the secondary containment enclosure. Specifically, these include a capability to: (a) maintain an effective barrier for gases and vapors that may leak from the primary containment during all normal and abnormal events; (b) delay the release of any gases and vapors that may leak from the primary containment during accidents; (c) allow gases and vapors that may leak through the primary containment during accidents to flow into the contained air volume within the secondary containment where they are diluted, held up, and purified prior to being released to the environs; (d) bleed to the secondary containment each air-filled containment penetration enclosure which extends beyond the Shield Building and which is formed by automatically actuated isolation valves; (e) maintain an effective barrier for airborne radioactive contaminants, gases, and vapors originating in the ABSCE during normal and abnormal events. | |||
Refer to Sections 3.8.1 and 3.8.4 for further details relating to the design of the Shield Building and the Auxiliary Building. | |||
6.2.3.1.2 Emergency Gas Treatment System (EGTS) | |||
The design bases for the EGTS are: | |||
(1) To keep the air pressure within each Shield Building annulus below atmospheric pressure at all times in which the integrity of that particular containment is required. | |||
Design Bases 6.2.3-1 | |||
WATTS BAR WBNP-112 (2) To reduce the concentration of radioactive nuclides in annulus air that is released to the environs during a LOCA in either reactor unit to levels sufficiently low to keep the site boundary and low population zone (LPZ) dose rates below the 10 CFR 100 values. | |||
(3) To withstand the safe shutdown earthquake. | |||
(4) To provide for initial and periodic testing of the system capability to function as designed. | |||
6.2.3.1.3 Auxiliary Building Gas Treatment System (ABGTS) | |||
The design bases for the ABGTS are: | |||
(1) To establish and keep an air pressure that is below atmospheric within the portion of the buildings serving as a secondary containment enclosure during accidents. | |||
(2) To reduce the concentration of radioactive nuclides in air releases from the secondary containment enclosures to the environs during accidents to levels sufficiently low to keep the site boundary and LPZ dose rates below the 10 CFR 100 guideline values. | |||
(3) To minimize the spreading of airborne radioactivity within the Auxiliary Building following an accidental release in the fuel handling and waste packaging areas. ABGTS is not required to mitigate the consequences of a fuel handling accident. | |||
(4) To withstand the safe shutdown earthquake. | |||
(5) To provide for initial and periodic testing of the system capability to function as designed (See Chapter 14.0 for information on initial testing of systems). | |||
6.2.3.2 System Design 6.2.3.2.1 Secondary Containment Enclosures (1) Shield Building The principal components that function collectively to form a secondary containment barrier around the steel primary containment vessel are the Shield Building itself, the Shield Building penetration seals, the isolation valves installed in the penetrations to the Shield Building, and the Shield Building penetration leakoff facilities. | |||
Structure The Shield Building is a reinforced concrete structure that encloses the reactor's steel primary containment structure; it has a circular horizontal cross section and a shallow domed roof. The vertical center line of this building is 6.2.3-2 System Design | |||
WATTS BAR WBNP-112 also the vertical center line of the steel primary containment vessel. The inside diameter of this building was sized to provide an annular shaped air space between the two reactor enclosures that is approximately five feet wide. The total enclosed free air space between the two enclosures is approximately 396,000 cubic feet. | |||
Penetrations To ensure that the Shield Building provides a nearly leak tight enclosure for the primary containment structure all openings in the shield building penetrations are sealed. Typical mechanical piping or ventilation penetrations are equipped with a flexible membrane seal as shown in Figure 6.2.3-1. Mechanical penetrations are designed for a leakage rate no greater than 0.0052 cfm per square inch when secondary containment is at a minus 0.5 inch water gauge. The primary containment personnel hatch passes through the Shield Building and opens directly to the Auxiliary Building. This opening in the Shield Building wall is handled as an ordinary piping penetration and is provided with a flexible, double membrane seal as shown in Figure 3.8.2-5 (see Section 3.8.2). Personnel and equipment access doors to the secondary containment are treated as special cases and are provided with resilient seals as shown in Figures 3.8.4-21 through 3.8.4-23. (See Section 3.8.4 for descriptions of the personnel access doors and the equipment access doors.) The allowable leakage for each personnel access door is 0.5 cfm when secondary containment is at minus 1 inch water gauge, and 10 cfm for the equipment access hatch when secondary containment is at minus 0.75 inch water gauge. | |||
Air filled lines which must be isolated by automatic valve actuation and which penetrate both the primary containment and the shield building are considered more likely to pass airborne radioactivities than other lines. | |||
Therefore these lines are provided with a third isolation valve outside the secondary containment for additional leak protection. This single, third valve receives both Train A and B actuation signals. Buffering prevents an electrical failure in one train from affecting the performance of the other train. | |||
To enhance the effectiveness of the third isolation valve as a barrier to leakage, the enclosed volume between the second and third isolation valves is opened to the annulus at all times. Opening this enclosed space to the annulus is accomplished with leakoff facilities as shown in Figure 6.2.3-2. | |||
This allows the negative pressure in the annulus to include this small volume, and leakage from the primary containment outward or leakage from outside the Shield Building inward to be drawn into the annulus for processing. The lines provided with this feature are those for the primary containment purge supply and exhaust. The 8-inch lower compartment pressure relief line is excluded from this consideration since it terminates in the annulus through a filter train and does not go outside the Shield Building. | |||
Electrical penetrations are of either a cable tray/cable slot type or a conduit type. Typical seals for these penetrations are shown in Figure 6.2.3-3. For System Design 6.2.3-3 | |||
WATTS BAR WBNP-112 cable tray/cable slot penetrations, silicone room temperature vulcanizing (RTV) foam is used as the sealant around cables within the wall opening over a portion of the length of the cable slot penetration. In conduit penetrations, the interstitial spaces between cables and conduit or condulet walls are filled with RTV silicone rubber as the sealant over a portion of the length of the penetration. Electrical penetrations are designed for a leakage rate not greater than 0.014 cfm per square inch when secondary containment is at a minus 0.5 inch water gauge. | |||
The total expected infiltration rate across all leakage paths into the annulus is 250 cfm at the post accident annulus control setpoint for a postulated single failure of one EGTS train (see Section 6.2.3.3.2 for a discussion of infiltration rate associated with a postulated single failure of one pressure control train). | |||
During normal operation the annulus pressure is maintained at or more negative than 5.0 inches water gauge with respect to the outside atmosphere. Periodic tests demonstrate that inleakage is less than this value. | |||
The fraction of primary containment leakage which may bypass the Shield Building and go directly to the Auxiliary Building is specified to be no greater than 25% of the total primary containment out-leakage. Permitting this leakage fraction results in acceptable site boundary and LPZ doses for the LOCA condition as described in Chapter 15. There are no significant paths by which primary containment leakage may bypass both the Shield Building and the Auxiliary Building and result in exceeding the offsite dose limits. | |||
Information concerning isolation features utilized in support of the secondary containment is presented in Section 6.2.4. Potential leakage paths by which primary containment leakage could bypass the secondary containment, and measures utilized to prevent such leakage are also discussed in Section 6.2.4. | |||
(2) Auxiliary Building Structure The Auxiliary Building provides an isolation barrier during certain postulated accidents involving airborne radioactive contamination. Certain of the buildings interior and exterior walls, floor slabs, and a part of its roof form the isolation barrier as shown in Figures 6.2.3-4 through 6.2.3-10. The enclosed volume of this isolation barrier, the ABSCE, is approximately 6.9 x 106 cubic feet. The ABSCE is discussed in more detail in Section 3 below. Additional data on the Auxiliary Building is provided in Section 3.8.4 and Table 6.2.3-1. | |||
(3) Auxiliary Building Secondary Containment Enclosure (ABSCE) | |||
The Auxiliary Building secondary containment enclosure (ABSCE) is that portion of the Auxiliary Building and CDWE Building (and for certain configurations, the annulus and primary containment, as discussed below) 6.2.3-4 System Design | |||
WATTS BAR WBNP-112 which serves to maintain an effective barrier for airborne radioactive contaminants released in the auxiliary building during abnormal events. | |||
Mechanical and electrical penetrations of this enclosure are provided with seals to minimize infiltration. Piping penetrations are either analyzed to pressure boundary retention requirements, or the effects of their failure are demonstrated not to impair the ability of the ABGTS system to maintain the ABSCE under the required negative pressure of 0.25 inches w.g., or they are isolated by physical means (e.g., locked-closed valves, etc.) Airlock-type doors are provided at portals where needed by the frequency of use. The negative pressure is maintained within the ABSCE to ensure that no contaminated air is released to the environs following an abnormal event without first being processed by the ABGTS. The ABSCE is shown in Figures 6.2.3-4 though 6.2.3-9. | |||
Entrances and exits to those portions of the Auxiliary Building within the primary containment barrier for both equipment and personnel are through air locks. The air lock locations are shown in Figures 1.2-3 and 1.2-5. The doors in each air lock are electrically interlocked such that only one side of the air lock can be opened at a time. A control room alarm is provided should both sides of an air lock ever be opened simultaneously. As a safety precaution, an interlock defeat switch is mounted on the containment side of each air lock to allow emergency egress should either side of the air lock be blocked open in an accident. | |||
A special case is the interlock system for the large exterior door to the railway loading area. When the large railroad access door is open, ABSCE airlock doors, such as the doors to the Post Accident Sampling Facility (PASF) and nitrogen storage area nor the access hatches above can be opened, and when either of these two doors and either of the access hatches above are open, the large railway access door cannot be opened. Administrative controls are provided to control doors and hatches during normal operation. | |||
The railway access doors and hatches are described in Section 3.8.4. | |||
The total permissible leakage rate for the ABSCE at a pressure of -0.25 inches water gauge with respect to the outside is 9900 cfm maximum. This represents 165.5% of the ABSCE free volume per day. Periodic tests demonstrate that inleakage is less than the design value. Any improvement in the inleakage recorded during subsequent tests shall be used to establish the allowable margin for breaching permits. | |||
During periods when the primary containment and/or annulus of both units are open to the Auxiliary Building, the ABSCE also includes these areas. A Containment Isolation Phase A (SI Signal) from the operating unit or high temperature in the Unit 1 or Unit 2 Auxiliary Building air intake, or manual ABI will cause a CVI signal in the refueling unit. These actions will ensure proper operation of the ABSCE. Both doors of the containment vessel personnel airlocks may be open at the same time during refueling activities while the purge air ventilation system is operating. During fuel handling operations in System Design 6.2.3-5 | |||
WATTS BAR WBNP-112 this configuration, a high radiation signal from spent fuel pool radiation monitors will result in a Containment Ventilation Isolation (CVI) in addition to an Auxiliary Building isolation and ABGTS start. Similarly, a CVI signal, including a CVI signal generated by a high radiation signal from the containment purge air exhaust radition monitors, will initiate an Auxiliary Building isolation and start of ABGTS. These are not required functions for the ABGTS and the Reactor Building Purge Systems filters or for Purge System isolation as no credit for these features is in mitigating a fuel handling accident. In the case where containment of both units is open to the Auxiliary Building spaces, a CVI in one unit will initiate a CVI in the other unit in order to maintain those spaces open to the ABSCE. | |||
Doors and penetrations of the ABSCE perimeter are provided with seals to reduce infiltration. Doors and hatches entering the area are either locked or under administrative control. | |||
Automatic redundant isolation dampers are provided in ducts which pass from areas inside the ABSCE to areas outside of the enclosure. These permit isolation of the ABSCE and allow the ABGTS to maintain a negative pressure in the area following an abnormal event. | |||
The ABGTS maintains a negative pressure with respect to the outside in the ABSCE during emergency operation and processes the Auxiliary Building exhaust. Either train of the ABGTS may be used to maintain the negative pressure and treat air exhausted from the ABSCE. | |||
The annulus vacuum control subsystem continues to operate whenever the ABSCE is isolated, except for a Phase A containment isolation signal. A Phase A containment isolation signal which is generated by a LOCA starts the air cleanup subsystem of the emergency gas treatment system. | |||
Calculations have shown that this condition does not result in exceeding the limits given in 10 CFR 100. For additional description of the annulus vacuum control subsystem of the EGTS, see Section 6.2.3.2.2. | |||
Proper actuation of the isolation dampers associated with the ABSCE and operation of the ABGTS is confirmed periodically. | |||
6.2.3.2.2 Emergency Gas Treatment System (EGTS) | |||
The EGTS is shown schematically in Figure 6.2.3-11. The logic and control diagrams for this system are shown in Figures 6.2.3-12 to 6.2.3-15A. This system has two subsystems: the annulus vacuum control subsystem and the air cleanup subsystem. | |||
The portions of the EGTS necessary to ensure that the system performs its functions during post-accident operation are classified Seismic Category I. Portions of the system which are not necessary for post-accident operation are seismically qualified to the extent that the system does not adversely affect any safety-related system(s)/component(s) as a result of its failure due to the seismic event; that is qualified Seismic Category I(L). | |||
6.2.3-6 System Design | |||
WATTS BAR WBNP-112 Annulus Vacuum Control Subsystem The annulus vacuum control subsystem is a fan and duct network used to establish and keep a negative pressure level within the annular space between the primary and secondary containment structures. It is utilized during normal operations in which containment integrity is required. In emergencies in which containment isolation is required, this subsystem is isolated and shut down. This subsystem performs no safety-related function. Because of this, the annulus vacuum control subsystem is not classified as an engineered safety feature. | |||
This subsystem has two independently controlled branches. Each branch serves one reactor unit. These branches draw air from their assigned annuli and release it into the Auxiliary Building Fuel Handling Area exhaust duct system. The air inlet for each branch is centrally located in its respective secondary containment volume above the steel containment dome. | |||
Air pressure control in each secondary containment annulus is achieved with one of the two, 100% capacity redundant fans, a differential pressure sensor, motor operated damper and control circuitry installation incorporated into each branch. This equipment provides a capability to vary the volumetric flow rate drawn from the annulus to keep the pressure at a predetermined negative pressure level. This control function is accomplished with a modulating damper under control of a differential pressure sensor that adjusts the amount of outside air introduced upstream of a constant capacity fan in the proper manner to keep the annulus pressure within a designated narrow range. One of the two redundant units starts automatically in the event the operating control unit fails to function in the proper manner. | |||
The fans and flow control dampers serving the reactor secondary containment annulus are installed in the EGTS room at Elevation 757.0' adjacent to the Unit 2 Shield Building. | |||
The nominal negative pressure for the annulus vacuum control equipment installation is 5 inches of water gauge. The controller setpoint is established such that the annulus pressure is maintained at, or more negative than, 5 inches water gauge. This negative pressure level chosen for normal operation ensures that the annulus pressure will not reach positive values during the annulus pressure surge produced by a LOCA in the primary containment. Two 100% capacity fans are utilized to maintain this negative pressure. One fan is normally on standby. | |||
Annulus vacuum control subsystem aids in containment pressure relief by exhausting the containment vent air after it goes through the containment vent air clean up units and is discharged into the annulus then into the Auxiliary Building exhaust stack (See Section 9.4.6). | |||
Air Cleanup Subsystem The air cleanup subsystem is a redundant, shared airflow network having the capability to perform two functions for the affected reactor secondary containment during a LOCA. One of these is to keep the secondary containment annulus air volume below System Design 6.2.3-7 | |||
WATTS BAR WBNP-112 atmospheric pressure. The second function is to remove airborne particulates and vapors that may contain radioactive nuclides from air drawn from the annulus. Each of these is accomplished by this subsystem without disturbing operation of the unaffected reactor unit. | |||
Both of these functions are performed by processing and controlling a stream of air taken from the reactor unit secondary containment annulus. The air cleanup operation is conducted by drawing the air stream through a series of filters and adsorbers. | |||
Annulus air pressure control is accomplished by adjusting the fraction of the airstream that is returned to the annulus air space. | |||
The negative pressure control setpoint chosen for post-accident operation is low enough that leakage across the boundary is into the annulus from both the primary containment and areas adjacent to the Shield Building. The pressure differentials produced by wind effects are also overcome by appropriate selection of the annulus negative pressure level. | |||
The rated capacity of each redundant air cleanup unit in the subsystem is 4000 cfm. | |||
This subsystem of the EGTS is classified as an engineered safety feature. | |||
The air flow network for the air cleanup subsystem was designed to provide the redundant services needed for either reactor secondary containment annulus. The suction-side ductwork in this network which is used to bring annulus air to the EGTS room on Elevation 757.0' in the Auxiliary Building is also used by the annulus vacuum control subsystem. The intake is centrally located within the Shield Building above the steel containment dome. Within the EGTS room the network branches out in a manner to supply two air cleanup unit installations that can be aligned with flow control dampers to serve either annulus air volume. After the air is processed through the air cleanup subsystem, it is routed to the redundant damper controlled flow dividers in the annulus. Inside each annulus, the air flow network contains two air flow paths: one leading to the Shield Building vent and the other to a manifold that distributes and releases the air uniformly around the bottom of the annulus. | |||
The vertical separation between the intake above the dome and the exhaust ports in the manifold is approximately 168 feet. Butterfly valves, rather than dampers, are installed in the ducts just above the flow distribution manifold to minimize the outside air inleakage from the reactor unit vents into the annulus. | |||
Another feature incorporated into the air cleanup subsystem air flow network is the capability to cool the filters and adsorbers in an inactive air cleanup unit that is loaded with radioactive material. This is accomplished with two cross-over flow ducts that can draw air at a minumum of 200 cfm from the active air cleanup unit through the inactive air cleanup unit. (Such an air flow is sufficient to keep the temperature rise through a fully loaded inactive air cleanup unit to less than 75°F.) Two butterfly valves in series are installed in each cross-over air flow path to assure sufficient isolation to perform accurate removal efficiency tests on the HEPA filter and carbon absorber banks. This feature is provided in the event excessive adsorber bed temperature occurs following the failure of an operating EGTS train. Adsorber bed temperature is indicated and 6.2.3-8 System Design | |||
WATTS BAR WBNP-112 supplied to the plant process computer. Status indication of each EGTS train is also provided. Upon failure of an operating EGTS train, adsorber bed temperature is monitored to detect subsequent temperature rise. After a Phase A containment isolation signal has initiated EGTS operation, the control room operator will shut one of the two EGTS trains down and align the appropriate butterfly valves for automatic operation. In addition, the associated suction valve is remotely opened from the main control room to establish a flow path from the annulus through the air cleanup unit. | |||
The two air cleanup units in the air cleanup subsystem have stainless steel housings containing air treatment equipment, sampling ports, heaters, drains, test fittings, and access facilities for maintenance. See Section 6.5.1.2.1 for a description of the air cleanup units and information related to their design. | |||
A centrifugal fan is provided outside each air cleanup unit housing. These fans were designed to function in process air flow streams at temperatures up to 200°F. See Table 6.2.3-1 for additional information on these fans. | |||
Two air flow control modules are also included in the air cleanup subsystem. Each consists of a differential pressure sensor and transmitter, control circuitry, a damper actuator, and two modulating dampers. The single damper actuator adjusts the dampers simultaneously in opposite directions, i.e., one is closed as the other is opened. | |||
A pressure control system with a station located in the main control room modulates pressure control dampers in the annulus to maintain the differential pressure setpoint. | |||
Two sets of independent pressure control dampers installed in the secondary containment annulus provide the capability to adjust the amount of air recirculated to the reactor unit annulus or discharged to the shield building exhaust vent. Annulus pressures that are more positive than the pressure controller setpoint produce a signal causing the damper actuator to begin closing the damper controlling the air flow to the annulus and to start opening the damper controlling the air flow to the Shield Building exhaust vent. Annulus pressures that are more negative than the pressure controller setpoint initiate the opposite kind of damper motions. | |||
Four isolation valves (two valves per train) installed in the secondary containment annulus provide isolation of the pressure control dampers. Each train has a handswitch in the control room positioned so that both trains of isolation valves are in A-AUTO . A containment isolation Phase A signal causes the valves to open. The open isolation valves provide a flow path for both trains of pressure control dampers which modulate to control annulus pressure. For further details, see Figures 6.2.3-14 and 6.2.3-15. | |||
Operation of the air cleanup subsystem during accidents is initiated by the Phase A containment isolation signal. Both the A and the B trains start and damper alignment initiated by this signal. A capability is also provided to start each fan with a hand switch in the main control room. Damper alignment is also initiated by the same signal. | |||
Another adjustment of hand switches in the main control room changes the operating mode to the single train operation with the redundant fan in a standby status. | |||
System Design 6.2.3-9 | |||
WATTS BAR WBNP-112 Employment of this operating mode is required after 1 hour and before 2 hours of operation. The control room operator can select either train to remain in operation. | |||
6.2.3.2.3 Auxiliary Building Gas Treatment System (ABGTS) | |||
The ABGTS is a fully redundant air cleanup network provided to reduce radioactive nuclide releases from the secondary containment enclosure during accidents. It does this by drawing air from the fuel handling and waste packaging areas through ducting normally used for ventilation purposes to air cleanup equipment, and then directing this air to the reactor unit vent. In doing so, this system draws air from all parts of the ABSCE to establish a negative pressure region in which virtually no unprocessed air passes from this secondary containment enclosure to the atmosphere. | |||
During periods when the primary containment and/or annulus of both units are open to the Auxiliary Building, the ABSCE also includes these areas. The ABGTS has been designed to establish a negative pressure in these additional areas for this configuration. During fuel handling operations in this configuration, a high radiation signal from the spent fuel pool radiation monitors will result in a Containment Ventilation Isolation (CVI) in addition to an Auxiliary Building isolation and ABGTS start. Similarly, a CVI signal, including a CVI signal generated by a high radiation signal from the containment purge air exhaust radiation monitors, will initiate an Auxiliary Building isolation and start of ABGTS. Likewise, a Containment Isolation Phase A (SI Signal) from the operating unit or high temperature in the Unit 1 or Unit 2 Auxiliary Building air intake, or manual ABI will cause a CVI signal in the refueling unit. These actions will ensure proper operation of the ABSCE. However, as an added precaution to protect the ABGTS operational boundary, operational action is needed to ensure the closure of the containment purge exhaust isolation valves (system valves not containment isolation valves) which are controlled by hand switches. In the case where containment of both units is open to the Auxiliary Building spaces, a CVI in one unit will initiate a CVI in the other unit in order to maintain those spaces open to the ABSCE. | |||
Although the ABGTS is available to minimize the consequences of a fuel handling accident, it is not required to function in order to meet control room and offsite dose limits based on the use of the Regulatory Guide 1.183, Revision 0 (Alternate Source Term) methodology. | |||
The portions of the ABGTS that are required to ensure that the system functions properly are classified Seismic Category I. Certain portions of the system, which are not required for post-accident operation of the ABGTS, are seismically qualified to the extent that system operation is not adversely affected should they fail due to the seismic event (i.e., classified according to Seismic Category I(L)). | |||
The rated capacity of each redundant ABGTS air cleanup unit (ACU) is 9000 cfm. | |||
These ACUs were designed in accordance with engineered safety feature standards. | |||
The unique portions of the ABGTS are shown schematically in Figures 6.2.3-16 and 9.4-8. Logic and control diagrams for the ABGTS are shown in Figures 9.4-10 and 9.4-17. The airflow network for this system consists of the exhaust ductwork, which normally serves the fuel handling and waste packaging areas connected to the 6.2.3-10 System Design | |||
WATTS BAR WBNP-112 suction-side of the Train A ACU, and a cross-over duct which connects the ductwork with the suction-side of the Train B ACU. The discharges from the Train A and Train B ABGTS exhaust fans separately go to the Unit 1 and Unit 2 Shield Building exhaust vents, respectively. | |||
The air flow ductwork that is not unique to this system consists of some of the normal ventilation ducting installed in the ABSCE. When the ABSCE is isolated, this duct network provides a flow path for the ABGTS to draw down and maintains a negative pressure in ABSCE. In some instances, air is drawn in the opposite direction to the normal air flow pattern during operation of the ABGTS. Each ACU includes air treatment components, instrumentation, test fittings, and other equipment required for proper operations and testing of the system. Refer to Section 6.5.1.2.2 for a description of the ABGTS air cleanup units and information related to their design. | |||
(1) | Information on these fans is given in Table 6.2.3-1. | ||
The air flow control modules utilized in the ABGTS contain a differential pressure sensor and transmitter, control circuitry, and a modulating damper. These air flow control modules provide the capability for keeping the pressure within the ABSCE at a minimum of 1/4 inch water gauge below atmospheric with the differential pressure transmitter and differential pressure controller circuit adjusting the amount of outside air admitted into the duct network by the vacuum relief line. Such action brings in sufficient outside air to keep the fan flow rate at its rated flow at all times. | |||
The negative pressure level chosen for post-accident operation is sufficiently low to ensure that airborne contamination present in the Auxiliary Building is not released to the environs without being processed by an air cleanup assembly. External pressure gradients produced by outside temperature and wind loadings on the building do not adversely affect the ability of the ABGTS to maintain the negative pressure in the ABSCE. | |||
The controls for the ABGTS are designed to provide two basic control modes. One control mode has either one of the air cleanup units in operation and the other in a state in which the redundant unit can automatically come into operation in the event the operating unit fails. Less negative than adequate pressure in the ABSCE is utilized in this control mode to make this failure determination. This operational redundancy is achieved with spatially separated power and control circuitry having different independent power sources to prevent a loss of function from any single system component failure. The term "Train A" is used to identify one complete set of full capacity equipment and the term "Train B" is used to identify the other set of full capacity equipment. Power for both equipment trains is supplied by the emergency power system. | |||
Operation of the ABGTS begins automatically upon initiation of an high radiation signal from the spent fuel pool accident radiation monitors or an ABI signal which is generated from one of the following signals: | |||
(1) Phase A containment isolation signal, or System Design 6.2.3-11 | |||
WATTS BAR WBNP-112 (2) High temperature signal from the Unit 1 and Unit 2 Auxiliary Building air intakes. | |||
Additionally, during refueling operations when containment and/or the annulus is open to the Auxiliary Building ABSCE spaces, a containment vent isolation signal from either the operating unit or refueling unit will automatically start the ABGTS. | |||
A capability is also provided to start each train with a hand switch (one hand switch per train) in the main control room. Another adjustment capability provided in the hand switches in the main control room changes the operating mode to the single train operation with the redundant train in a standby status. Employment of this operating mode is expected after the first 30 minutes of operation. In this instance, the main control room operator has the capability to select either train to remain in operation. | |||
(1) | The standby unit selected automatically starts in the event the operating unit does not adequately maintain negative pressure in the ABSCE. | ||
6.2.3.3 Design Evaluation 6.2.3.3.1 Secondary Containment Enclosures The secondary containment enclosures are designed to provide a positive barrier to all potential primary containment leakage pathways during a LOCA and to radioactive contaminants released in accidental spills and fuel handling accidents that may occur in the ABSCE. In a LOCA, the Shield Building containment enclosure provides the barrier to all airborne primary containment leakage, and the ABSCE provides a barrier to through-the-line leakage which can potentially become airborne. The ABSCE also maintains an effective barrier for airborne radioactive contaminants originating inside the ABSCE during normal and abnormal events. The original design credited the secondary containment enclosures to mitigate the consequences of a FHA. Although these enclosures are available to minimize the consequences of a FHA, based on the use of the Regulatory Guide 1.183, Revision 0 (Alternate Source Term) methodology for a FHA, the structures are no longer required for mitigation of a postulated FHA. | |||
(1) Shield Building Structure The Shield Building provides the physical barrier for airborne primary containment leakage during a LOCA. Because the Shield Building completely encloses the free standing primary containment, most of the airborne leakage from primary containment passes into the annular region provided by this arrangement. | |||
The building construction employs monolithic pours of concrete. This approach for structures of this type produces a very low leakage barrier. The low leakage characteristics of this barrier help to reduce the rate at which purified annulus air must be released to maintain the enclosed volume at a negative pressure. This factor contributes significantly to keeping the site boundary and the low population zone (LPZ) dosage levels within 10 CFR 100 guidelines. | |||
6.2.3-12 Design Evaluation | |||
WATTS BAR WBNP-112 The design of the EGTS system and the size of the annular region between the primary containment and the shield building assures a residence time for all leakage into the annulus. | |||
Penetrations The Shield Building wall is provided with many penetrations to accommodate mechanical equipment piping, cable trays, and electrical conduit which leave and enter the Shield Building. Due to the low leakage characteristics of the building, leakage through the Shield Building wall is restricted almost entirely to openings in these penetrations. The design assures that penetration leakage does not exceed predetermined quantities. Such a capability ensures that the inleakage is sufficiently low to keep the dose contributions at the site boundary and to the LPZ within 10 CFR 100 guidelines. | |||
Openings in mechanical piping penetrations are sealed principally as shown in Figure 6.2.3-1. The seals are a flexible membrane type of single gaskets which incorporate fire resistant materials and are designed to withstand the combinations of Shield Building and piping movements in the SSE and retain their functional integrity. In addition, seals at or below the probable maximum flood elevation are designed to be water tight for flood static head and surge forces. All seals, where possible, are installed outside the Shield Building such that whether during normal operation, accidents, or flood, the differential pressures will tend to enhance the tightness of the seal. The penetration seal materials have been selected to be compatible with the maximum design integrated dose for the Shield Building during a LOCA. | |||
Cables routed in cable trays pass through the Shield Building wall through rectangular cable slot penetrations as shown in Figure 6.2.3-3. The sealant material installed around cables over a portion of the length of the cable slot is silicone RTV (room temperature vulcanizing) foam and is RTV silicone rubber installed around cables within conduits. The seals are typically shown in Figure 6.2.3-3 and are designed to withstand the SSE and retain their integrity. Electrical penetration seals are allowed twice the leakage of mechanical seals to provide sufficient margin in meeting the total allowable Shield Building leakage requirements. | |||
The personnel and equipment access doors to the Shield Building are designed with heat resistant, resilient seals which reduce their leakage to the allowable values as stated in Section 6.2.3.2. These doors are designed to retain their structural integrity and leak tightness during a SSE as described in Sections 3.8.1 and 3.8.2. | |||
To allow personnel access to the annulus during operation, the annulus personnel access doors form an airlock. The doors are electrically interlocked such that only one of the pair may be opened at a time, but an electric interlock defeat switch is provided inside the annulus to provide for emergency egress from the annulus Design Evaluation 6.2.3-13 | |||
WATTS BAR WBNP-112 should the door on the Auxiliary Building side of the lock be blocked open during an accident. Therefore, a continuous secondary containment barrier is provided while allowing personnel movement. | |||
The fuel transfer tubes penetrate the primary and secondary containment on their way to the Auxiliary Building. Each transfer tube has a blind flange on the inboard side of primary containment, equipped with double seals and a pressure test connection between the seals. The valve in the Auxiliary Building end of the transfer tube serves as the secondary containment isolation valve. The inner space between the primary containment flange and the isolation valve is bled to the annulus so that any leakage into the tube from primary containment or the Auxiliary Building flows into the annulus. The bleed line is routed above the maximum refueling pool water level to preclude accidental spills of refueling water. | |||
(2) Auxiliary Building Structure The entire Auxiliary Building including walls, roof, and interior partitions is constructed by consecutive monolithic pours of concrete. This method of assembly produces a structure with very low leakage characteristics. The portions of the building chosen to constitute the isolation barrier were selected such that sources of potential contamination are completely enclosed. Therefore, the structure utilized to form the Auxiliary Building containment envelope functions effectively as a barrier to the environs. This same structure also helps to reduce inleakage into the Auxiliary Building containment envelope during accidents to levels easily accommodated by the ABGTS. | |||
Penetrations Seals for mechanical penetrations are a flexible membrane type or single gaskets. The seals are designed to withstand Auxiliary Building and piping movements in the SSE and retain their structural integrity. The materials chosen for the seals are fire resistant. The seals, where possible, are designed such that whether during normal operation or accidents, the differential pressures tend to enhance the tightness of the seal. Sealing methods for electrical penetrations are similar to those for the Shield Building electrical penetrations. | |||
Each normal ventilation duct penetrating the ABSCE is equipped with two isolation dampers in series. The dampers have resilient blade end and blade edge seals which are designed to retain their functional characteristics. The motor operators for these dampers have been sized to tightly close the damper blades against their resilient seals. The damper and motor operator assemblies are designed to operate during and after the SSE. | |||
6.2.3-14 Design Evaluation | |||
WATTS BAR WBNP-112 Piping penetrations are analyzed to pressure boundary retention requirements. | |||
The effects of piping penetration failures are demonstrated to not impair the ability of the ABGTS system to maintain the ABSCE pressure boundary (under the required negative pressure of 0.25 inches w.g.), or the penetrations are isolated by physical means (e.g., locked-closed valves). | |||
6.2.3.3.2 Emergency Gas Treatment System (EGTS) | |||
The EGTS has the capabilities needed to preserve safety in accidents as severe as the design basis LOCA. To verify that the proper features are provided, functional analyses were conducted which consist of failure modes and effects analysis of the system, reviews of Regulatory Guide 1.52 sections to assure licensing requirement conformance, and performance analyses to verify that the system has the desired accident mitigation capabilities. A detailed failure modes and effects analysis is presented in Table 6.2.3-2. The system is shown schematically in Figure 6.2.3-11. | |||
The functional analyses conducted on the EGTS have shown that: | |||
(1) Adequate isolation of the annulus vacuum control subsystem during accidents is provided. The two low leakage valves in series upstream of the annulus vacuum control subsystem fans used to isolate the two subsystems--one operated by each subsystem train--give assurance that the annulus vacuum control subsystem will be isolated during accidents. These valves fail closed. | |||
(2) The air flow control dampers in the air cleanup subsystem align to service the affected reactor units. The network was designed to have the air flow control dampers shown in Figures 6.2.3-18 and 6.2.3-19 needed to service a particular reactor unit responsive to only the containment isolation signal from that particular reactor unit. | |||
(3) The system intake and recirculation air outlets, shown on Figures 6.2.3-18 and 6.2.3-19, within the Shield Building annulus are positioned to promote mixing and dilution of primary containment leakage. Positioning the recirculation air manifold and the air outlets almost completely around the base of the annulus below the level of the containment penetrations assures a clean air flow past most of the penetrations. This air, warmed by the relative humidity heater, flows upward past these likely sources of leakage. In doing so, the flow impediments (i.e., penetrations, and structures within the annulus) tend to redirect this air flow to induce mixing and dilution. | |||
6.2.3.3.2 | |||
(1)Adequate isolation of the annulus vacuum control subsystem during accidents is provided. The two low leakage valves in series upstream of the annulus vacuum control subsystem fans used to isolate the two subsystems--one operated by each subsystem train--give assurance that the annulus vacuum control subsystem will be isolated during accidents. These valves fail closed. | |||
(2)The air flow control dampers in the air cleanup subsystem align to service the affected reactor units. The network was designed to have the air flow control dampers shown in Figures 6.2.3-18 and 6.2.3-19 needed to service a particular reactor unit responsive to only the containment isolation signal from that particular reactor unit. | |||
(3)The system intake and recirculation air outlets, shown on Figures 6.2.3-18 and 6.2.3-19, within the Shield Building annulus are positioned to promote mixing and dilution of primary containment leakage. Positioning the recirculation air manifold and the air outlets almost completely around the base of the annulus below the level of the containment penetrations assures a clean air flow past most of the penetrations. This air, warmed by the relative humidity heater, flows upward past these likely sources of leakage. In doing so, the flow impediments (i.e., penetrations, and structures within the annulus) tend to redirect this air flow to induce mixing and dilution. | |||
Substantial amounts of mixing and dilution are likely in the vertical rise of over 168 feet to the system air intake above the steel containment dome. | Substantial amounts of mixing and dilution are likely in the vertical rise of over 168 feet to the system air intake above the steel containment dome. | ||
(4)System startup reliability is very high. The practice of automatically starting up both full capacity trains in the system simultaneously gives greater assurance that one train of equipment functions promptly upon receipt of an accident signal. | (4) System startup reliability is very high. The practice of automatically starting up both full capacity trains in the system simultaneously gives greater assurance that one train of equipment functions promptly upon receipt of an accident signal. | ||
Design Evaluation 6.2.3-15 | |||
Design Evaluation 6.2.3- | |||
WATTS BAR WBNP-112 (5) The use of a single actuator in each equipment train to adjust dampers controlling the air flow recirculated and vented improves train reliability and minimizes the possibility of annulus pressure instability. Simultaneous adjustment that closes one damper and opens the other eliminates the hunting problems that could arise from nonsimultaneous operation of separately actuated dampers. | |||
(6) The Train A and Train B air cleanup units are adequately protected from each other to eliminate the possibility of a single failure destroying the capability to process annulus air during emergencies. The 13.5 feet high and 27 inch thick concrete wall built between the two units protects each from missiles originating in the other unit. | |||
The EGTS, designed prior to issuance of Regulatory Guide 1.52, is in general agreement with requirements in the guide. Details on this compliance with Regulatory Guide 1.52 are given in Table 6.5-1. | |||
The performance analyses conducted to verify that the EGTS has the required accident mitigation capabilities were conducted in three basic parts. One of these was concerned with the capability for keeping the Shield Building annulus below atmospheric pressure at all times during a LOCA. The second part was an analysis of the cooling capabilities provided to keep temperatures within filters and adsorbers fully loaded with radioactive nuclides at safe levels. The third part was concerned with the site boundary and LPZ dosage contribution from radioactive nuclides present in annulus air releases during the design basis LOCA. These three analyses are discussed under the respective headings below. | |||
Annulus Negative Pressure Control Capability The capability of the EGTS to keep the Shield Building annulus below atmospheric pressure during a design basis LOCA was established with a time iteration analysis performed by a computer. Energy and mass balances were accomplished successively in accordance with mass and volume changes calculated to take place during each time increment. Such a methodology allowed sufficient freedom to account for: | |||
(1) Steel containment vessel growth from internal pressure, (2) Steel containment vessel growth from thermal expansion, (3) Outside air inleakage into the Shield Building annulus, and (4) Heat transfer from the steel containment structure to the annulus air mass. | |||
To assure that this analysis was valid and conservative: | |||
(1) Heat transfer from the primary containment atmosphere to the primary containment vessel was assumed to be convective. An air-steam mixture convective heat transfer coefficient was chosen to maximize heat transfer to 6.2.3-16 Design Evaluation | |||
WATTS BAR WBNP-112 the secondary containment atmosphere. The constant value of 400 Btu/hr-ft2-°F given in Table 6.2.3-1 compares conservatively to the integrated transient heat transfer coefficients recommended in Branch Technical Position CSB 6-1. Heat transfer from the primary containment vessel to the annulus atmosphere and from the atmosphere to the secondary containment wall was assumed to be convective. Heat transfer from the primary containment vessel to the secondary containment wall was assumed to be by radiation. Forms of the transient convective heat transfer coefficients and values for the constant radiative heat transfer coefficients are given in Table 6.2.3-1. Consideration was given to the heat capacity of both the primary and secondary containment structures. The thermal conductivity and capacitance for these walls, as given in Table 6.2.3-1, agree closely with those obtained from Branch Technical Position CSB 6-1. | |||
6.2.3- | (2) The thermal growth of the steel vessel was based on linear expansion which was applied to the transient containment vessel temperature increases above the initial steady-state values to obtain the transient radial expansion (see Table 6.2.3-1 for total containment expansion). Temperature gradients were calculated for three regions: upper compartment, ice condenser, and lower compartment. The radial expansions in each of these three regions were converted to volume changes which were summed to yield a total annulus volume change due to primary containment vessel thermal expansion. | ||
(3) Table 6.2.3-1 presents the characteristics of the internal pressure effects on the containment vessel. This model uses linear elastic thin shell theory to determine the expansion. The cylindrical portion of the vessel is assumed to act as a cylindrical shell with capped ends. The hemispherical dome expands uniformly as a simple sphere and includes the axial expansion of the cylinder. | |||
External vertical and circumferential stiffeners are assumed not to be present so that conservative results are obtained. This pressure-induced growth was assumed to occur instantaneously at the start of the LOCA. | |||
(4) Air leakage into the Shield Building annulus was assumed to be 250 cfm at the post accident annulus control setpoint for a postulated single failure of one EGTS train. A more conservative air inleakage value of 832 cfm was assumed for an alternate single failure scenario which results in one pressure control train in full exhaust to the shield building exhaust stack while the other train remains functional. This higher inleakage value is based upon the higher negative pressure that will exist within the annulus during this scenario. | |||
(5) The air temperature in the annulus was assumed to be a thermally mixed average. | |||
Design Evaluation 6.2.3-17 | |||
WATTS BAR WBNP-112 (6) Only one train of the EGTS was assumed to operate during the first single failure scenario, allowing for a possible single failure in the other. An alternate single failure scenario was analyzed which postulates one pressure control train failing which results in full exhaust to the shield building exhaust stack while the other train remains functional. | |||
The initial steady state conditions used in this analysis were as follows (refer also to Table 6.2.3-1): | |||
Relative Pressure Temperature Humidity Containment upper compartment atm. 110°F 0% | |||
Ice condenser compartment atm. 15°F 0% | |||
Containment lower compartment atm. 120°F 0% | |||
Shield Building annulus -5 in. w.g. 50°F 0% | |||
Outside atm. 0° 0% | |||
These initial values were chosen to maximize the secondary containment pressure after the LOCA. The initial pressure of minus 5.0 inches of water gauge with respect to the outside is the pressure maintained by the annulus vacuum control subsystem during normal operation. The initial temperature of 50°F is the estimated minimum temperature which was assumed for maximum annulus air density. Similarly, the initial relative humidity of 0% was assumed for maximum annulus air density for conservatism. | |||
The results obtained from this analysis for the first single failure scenario are shown in Figure 6.2.3-17. This annulus pressure and EGTS exhaust rate vs. time curve indicates that, after the initial containment pressure induced step increase, the pressure rises to a peak value of approximately minus 1.06 inch of water in about 79 seconds after the LOCA begins. The annulus pressure is then restored and maintained at or below the EGTS setpoint value as shown in Figure 6.2.3-17. | |||
The results obtained from the analysis for the alternate single failure scenario are shown in Figure 6.2.3-17A. This annulus pressure and EGTS exhaust rate vs. time curve indicates that, after the initial containment pressure induced step increase, the pressure rises to a peak value of approximately minus 1.52 inch of water in about 50 seconds after the LOCA begins. The annulus pressure is then restored and maintained at or below the EGTS setpoint value as shown in Figure 6.2.3-17A. | |||
The expansion of approximately 1,234 ft3 due to internal temperature summed with the expansion of 766 ft3 from internal pressure yields a total primary containment vessel expansion of approximately 2,000 ft3. Such results indicate that: | |||
6.2.3-18 Design Evaluation | |||
the | WATTS BAR WBNP-112 (1) The negative pressure level of 5 inches of water below atmospheric in the Shield Building annulus maintained by the annulus vacuum control subsystem before an accident minimizes the amount of unfiltered radioactive nuclides potentially released to the environment before the air cleanup subsystem becomes operational. | ||
(2) The rated flow rate of 4000 +/-10% cfm for each train of the air cleanup subsystem is adequate to keep the annulus pressure below the negative pressure setpoint throughout the remaining period of the LOCA. | |||
Inactive Air Cleanup Unit Cooling Capabilities The second performance analysis conducted to show that the EGTS can cope with circumstances that may occur in a LOCA was concerned with temperature control capabilities provided for air filters and adsorbers loaded with radioactive material. The analysis conducted assumed accident releases in accordance with Regulatory Guide 1.89 (100% noble gas activity, 50% iodines, and 1% particulates) and containment leakages of 0.25% per/day for the first day and 0.125% per/day from one to 100 days in accordance with Regulatory Guide 1.4. An additional assumption made was that the gamma and beta energy releases were transformed into heat within the filters and absorbers. | |||
This occurs a few days after the LOCA takes place. The design objective is to assure that the air cleanup unit component temperatures do not exceed 200°F; it was found that a cooling air flow rate of 112 cfm is required. Such results indicate that the cooling air flow rate of 200 cfm provided for this purpose should keep the temperature within the carbon adsorber bank well below the 620°F carbon ignition temperature. | |||
Site Boundary and LPZ Dosage Contributions The last performance analysis conducted to show that the EGTS has the capability to perform in the required manner to preserve safety during a LOCA was concerned with the site boundary and LPZ dosage contributions arising from annulus air releases to the environs. This analysis is described and evaluated in Chapter 15. | |||
6.2.3.3.3 Auxiliary Building Gas Treatment System (ABGTS) | |||
The ABGTS has the capabilities needed to preserve safety in accidents as severe as a LOCA. This was determined by conducting functional analyses of the system to verify that the system has the proper features for accident mitigation which consist of a failure modes and effects analysis, a review of Regulatory Guide 1.52 sections to assure licensing requirement conformance, and a performance analysis to verify that the system has the desired accident mitigation capabilities. A detailed failure modes and effects analysis is presented in Table 6.2.3-3. | |||
The functional analyses conducted on the ABGTS have shown that: | |||
(1) The air intakes for the system are properly located to minimize accident effects. The use of the air intakes provided in the fuel handling and waste disposal areas minimizes the spread of airborne contamination that may be Design Evaluation 6.2.3-19 | |||
the | WATTS BAR WBNP-112 accidentally released at these positions in which the probability of an accidental release, e.g., a fuel handling accident, is more likely. This localization effect is provided without reducing the effectiveness of the system to cope with multiple activity released throughout the ABSCE that may occur during a LOCA. Such coverage is accomplished by utilizing the normal ventilation ducting to draw outside air inleakage from any point along the secondary containment enclosure to the fuel handling and waste disposal areas. | ||
(2) Accident indication signals are utilized to bring the ABGTS into operation to assure that the system functions when needed to mitigate accident effects. | |||
Accidents in which this system is needed to preserve safety are automatically detected by at least one of the three instrumentation sets used to generate accident signals that result in system startup. | |||
(3) System startup reliability is very high. The practice of allowing the automatic startup of both full capacity trains in the system gives greater assurance that one train of equipment functions upon receipt of an accident signal. | |||
(4) The method adopted to establish and keep the negative pressure level within this secondary containment enclosure minimizes the time needed to reach the desired pressure level. Initially, the full capacity of the ABGTS fans is utilized for this purpose. After reaching the desired operating level, the system control module allows outside air to enter the air flow network just upstream of the fan at a rate to keep the fans operating at full capacity with the enclosed volume at the desired negative pressure level. In this situation, the amount of air withdrawn from the enclosed volume is equal to the amount of outside air inleakage through the ABSCE. In addition, two vacuum breaker dampers in series are provided to admit outside air in case the modulating dampers fail. | |||
(5) The ABSCE is maintained at a slightly negative pressure to reduce the amount of unprocessed air escaping from this secondary containment enclosure to the atmosphere to insignificant quantities. In addition, this negative pressure level is less than that which is maintained within the annulus; such that, any air leakage between the Auxiliary Building and the Shield Building is from the Auxiliary Building into the Shield Building. | |||
(6) The Train A and Train B air cleanup units are sufficiently separated from each other to eliminate the possibility of a single failure destroying the capability to process Auxiliary Building air prior to its release to the atmosphere. Two concrete walls and a distance of more than 80 feet separate the two trains. | |||
The use of separate trains of the emergency power system to drive the air cleanup trains gives further assurance of proper equipment separation. | |||
The review of the ABGTS conducted to determine its conformance with Regulatory Guide 1.52 has shown that this system, designed prior to issuance of the guide, is in 6.2.3-20 Design Evaluation | |||
WATTS BAR WBNP-112 general agreement with its requirements. Details on compliance with Regulatory Guide 1.52 are given in Table 6.5-2. | |||
The performance analysis conducted to verify that the ABGTS has the required accident mitigation capabilities has shown that the system flow rate is sized properly to handle all expected outside air inleakage at a 1/4-inch water gauge negative pressure differential. This indicates that the nominal flow rate of 9000 cfm is sufficient to assure an adequate margin above the expected ABSCE inleakage (ACU filters are replaced as needed to maintain a minimum flow capability of 9300 cfm under surveillance instructions). | |||
The performance analysis evaluated the capability of the ABGTS to reach and maintain a negative pressure of 1/4-inch water gauge with respect to the outside within the boundaries of the ABSCE. The following was utilized in the analysis: | |||
(1) Leakage into the ABSCE is proportional to the square root of the pressure differential. | |||
(2) Only one air cleanup unit in the ABGTS operates at the rated capacity. | |||
(3) The air cleanup unit fan begins to operate 30 seconds after the initiation of an ABI signal. | |||
(4) The initial static pressure inside the ABSCE is conservatively considered to be atmospheric pressure, although the ABSCE is under a negative pressure during normal operation. | |||
(5) The effective pressure head due to wind equals 1/8-inch water gauge. | |||
(6) Initial average air temperature inside the ABSCE equals 140°F. | |||
(7) Atmospheric temperature and pressure are 70°F and 14.4 psia, respectively. | |||
(8) ABSCE isolation dampers/valves close within 30 seconds after receiving an ABI signal. | |||
(9) The non-safety-related general ventilation and fuel handling area exhaust fans are designed to shut down automatically following a LOCA. Each fan is provided with a safety related Class 1E primary circuit breaker and a safety related Class 1E shunt trip isolation switch which is tripped by a signal of the opposite train from that for the primary circuit breaker to ensure that power is isolated from the fan. | |||
The analysis utilizes the first law of thermodynamics and perfect gas relations in an iterative approach to determine temperature and pressure changes in the ABSCE. | |||
Heat sources and sinks (ESF equipment room coolers) are considered. | |||
Design Evaluation 6.2.3-21 | |||
WATTS BAR WBNP-112 The results obtained indicate that the ABGTS has the capability to reach and maintain a negative pressure differential of 0.25 inches water gauge within four minutes of the receipt of an ABI signal. | |||
The system contains sufficient air cleanup facilities to keep the contributions to the site boundary and LPZ dosage arising from Auxiliary Building air releases to small fractions of the 10 CFR 100 guideline values. This part of the analysis is presented and evaluated in Chapter 15. | |||
6.2.3.3.4 Tritium Production Core Evaluation (Unit 1 Only) | |||
The effects of converting WBN to a Tritium Production Core (TPC) on the Secondary Containment design has been evaluated. The evaluation includes the effect of adding a leading edge flow meter (LEFM) into the main feedwater piping and the effect of uprating the plant nominal power level by 1.4%. | |||
Secondary containment is designed to have the capability to control the atmosphere within the secondary containment and contiguous areas during normal operation and during plant upset conditions. As explained in UFSAR Section 6.2.1.3.12, the current licensing basis mass and energy release bounds that of the TPC; therefore, the conversion to a TPC will not have any effect on the secondary containment functional design. | |||
6.2.3.4 Test and Inspections 6.2.3.4.1 Emergency Gas Treatment System (EGTS) | |||
Preoperational testing of the EGTS was conducted to verify that the Shield Building and the EGTS had the capabilities needed to keep LOCA generated activity releases from the affected reactor unit at or below limits specified in 10 CFR 100. Included in the scope of testing were functional tests on all system instrumentation, controls, and alarms. The tests were structured to accomplish the following: | |||
(1) Verification that Shield Building infiltration was less than or equal to the design value at the design negative pressure level for post-accident conditions. | |||
(2) Verification of the system capability to establish and maintain the proper negative pressure level in the annulus. | |||
(3) Verification that the air cleanup units met requirements specified in Regulatory Guide 1.52. Refer to Section 6.5.1.4.1 for further information related to tests applicable to the air cleanup units. | |||
(4) Verification of proper operation of all system components, instrumentation, alarms, and data displays. | |||
The periodic test program for the EGTS fans and air cleanup units is described in the Technical Specifications. A periodic test is performed once every 18 months to verify that the EGTS can maintain the annulus at a negative pressure within the instrument 6.2.3-22 Test and Inspections | |||
the | WATTS BAR WBNP-112 deadband immediately above and below the nominal design value. This test also verifies that the Shield Building inleakage rate to the annulus is less than or equal to 250 cfm at the nominal design value. A verification of system flow capacity and Shield Building inleakage rates at the specified negative pressure is adequate to confirm that the calculated depressurization time is conservative. The EGTS fans start within 30 seconds following the initiation of a containment isolation phase A signal. | ||
6.2.3.4.2 Auxiliary Building Gas Treatment System (ABGTS) | |||
Preoperational testing of the ABGTS was conducted to verify that the ABGTS has the capabilities needed to reduce radioactive releases from the ABSCE to the environment during an accident to levels sufficiently low to keep the site boundary dose rates below the requirements of 10 CFR 100. Included in the test scope were functional tests on all system instrumentation, controls, and alarms. The tests were structured to accomplish the following: | |||
(1) Verification of the system startup and control capabilities, considering a single operating component failure. | |||
(2) Verification of the capability of the air flow control modules to create and maintain a negative pressure within the ABSCE. | |||
(3) Verification that ABSCE infiltration rate was less than or equal to the design value at the design negative pressure level considering a postulated failure of a non-safety related component. | |||
(4) Verification that the air cleanup units met the requirements specified in Regulatory Guide 1.52. Refer to Section 6.5.1.4.2 for further information related to tests applicable to the air cleanup units. | |||
The periodic test program for the ABGTS fans and air cleanup units is described in the Technical Specifications. A periodic test is performed to verify that the ABGTS can maintain the ABSCE at a negative pressure between -0.25 and -0.5 inches of water with respect to atmospheric pressure. This test also verifies that the ABSCE vacuum relief flow rate is greater than or equal to 1370 cfm while the ABSCE is being maintained at the negative pressure described above. A verification of system flow capacity and ABSCE vacuum relief flow rate at the specified negative pressure is adequate to confirm that the calculated depressurization time is conservative. | |||
6.2.3.5 Instrumentation Requirements 6.2.3.5.1 Emergency Gas Treatment System (EGTS) | |||
The air flow control instrumentation requirements for the EGTS are described in Section 6.2.3.2.2. Instrumentation associated with the air cleanup units is discussed in Section 6.5.1.5.1. The logic, controls, and instrumentation of this engineered safety feature system are such that a single failure of any component does not result in the loss of functional capability for the system. | |||
Instrumentation Requirements 6.2.3-23 | |||
WATTS BAR WBNP-112 6.2.3.5.2 Auxiliary Building Gas Treatment System (ABGTS) | |||
Instrumentation required for the air flow control modules and air cleanup units are discussed in Section 6.2.3.2.3. Instrumentation associated with the air cleanup units is discussed in Section 6.5.1.5.2. The logic, controls, and instrumentation of this engineered safety feature system are such that a single failure of any component does not result in the loss of functional capability for the system. | |||
REFERENCES None 6.2.3-24 Instrumentation Requirements | |||
WATTS BAR WBNP-112 Table 6.2.3-1 Dual Containment Characteristics (Page 1 of 2) | |||
I. Secondary Containment Design Information Shield Bldg. ABSCE (Incl. 2 x Shield Bldg., 2 x Contmt., AB and CDWE Bldg.) | |||
A. Free Volume (ft3) 3.96 x 105 6.9 x 106 B. Pressure (in. wg)# | |||
Normal Operation -5.0 -0.25 Post-Accident -0.5 -0.25 C. Leak Rate at Post- Accident Pressure (%/day) 91 165.5 D. Exhaust Fans Normal Operation Number 4 (2/reactor unit)* 6** | |||
Type centrifugal centrifugal Post-Accident Operation Number 2*** 2**** | |||
Type centrifugal centrifugal E. Filters: Refer to Table 6.5-5 II. Transient Analysis A. Initial Conditions | |||
: 1. Pressure = 14.4 psig | |||
: 2. Annulus temperature = 50°F | |||
: 3. Outside air temperature = 0°F | |||
: 4. Thickness of secondary containment wall = 36 in. | |||
: 5. Thickness of steel containment vessel = ranging from 0.8125 to 1.50 inches | |||
* Annulus vacuum control subsystem | |||
**Auxiliary Building general exhaust (2/unit) and fuel handling area exhaust (2) | |||
***EGTS | |||
****ABGTS | |||
# Due to instrument locations and inaccuracies, the actual setpoints are more negative than the required values shown. | |||
Instrumentation Requirements 6.2.3-25 | |||
WATTS BAR WBNP-112 Table 6.2.3-1 Dual Containment Characteristics (Page 2 of 2) | |||
II. Transient Analysis (continued) | |||
: | B. Thermal Characteristics | ||
: 1. Primary containment wall | |||
: a. Total expansion = 2000 ft3 Pressure expansion = 766 ft3 Temperature expansion = 1234 ft3 | |||
: b. Thermal conductivity = 31 Btu/hr-ft-°F | |||
: c. Heat capacity = 0.111 Btu/lb-°F | |||
: 2. Secondary containment wall | |||
: a. Thermal conductivity = 1.6 Btu/hr-ft-°F | |||
: b. Heat capacity = 0.22 Btu/lb-°F | |||
: 3. Heat transfer coefficients | |||
: a. Primary containment atmosphere to primary containment wall = 400 Btu/hr-ft2-°F | |||
: b. Primary containment wall to secondary containment atmosphere = 0.19 (T)1/3 Btu/hr-ft2-°F | |||
: c. Secondary containment wall to secondary containment atmosphere = 0.19 (T)1/3 Btu/hr-ft2-°F | |||
: d. Primary containment emissivity = 0.90 | |||
: e. Secondary containment emissivity = 0.90 6.2.3-26 Instrumentation Requirements | |||
Instrumentation Requirements WATTS BAR Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System (Page 1 of 17) | |||
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS | |||
: 1. EGTS ACU Fans Draws air from the - Stops running - Electrical Low flow alarm in Reduction of flow None (See Remarks) Redundant fan starts on A-A & B-B annulus to maintain - Does not run Failure the MCR from annulus and low flow signal from failed negative pressure in temporary reduction fan and train. | |||
the annulus during - Mechanical in annulus negative design basis events Failure pressure Both trains of the EGTS system start on receipt of a Phase A isolation signal. | |||
However, operators will align the system to single train operation after a period of time. | |||
: 2. EGTS ACU Filters air to remove - Filters leak - Defective filters High radiation High radiation in None (See remarks) Periodic testing of EGTS A-A & B-B airborne particulates - Filters become levels indicated in shield building ACUs is conducted in and vapors from the loaded - High levels of the MCR from exhaust vent. accordance with R.G. 1.52 annulus during design radioactivity shield building to verify leak tightness of basis events contamination exhaust vent HEPA and charcoal bank efficiencies. High radiation | |||
- Large quantities levels are indicated in the of particulates MCR for operators to start the redundant ACU, if necessary. | |||
: 3. Containment Isolate annulus Open - Electrical Valve position None (See Remarks) None (See Remarks) Redundant valve in series annulus vacuum vacuum control fans Failure indication light in with failed valve provides control fan suction from EGTS during the MCR isolation function. | |||
isolation valves ACU operation - Mechanical failure 1-FCV-65-52 1-FCV-65-53 2-FCV-65-4 2-FCV-65-5 6.2.3-27 WBNP-112 | |||
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System 6.2.3-28 WATTS BAR (Page 2 of 17) | |||
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS | |||
: 4. B train isolation Provide decay heat Open (ACU A-A is - Electrical Valve position Parallel flow path to None (See Remarks) Additional flow path is valves at EGTS removal cooling flow in operation) failure indication light in ACU A-A is open available which causes no Train A suction path for A-A ACU the MCR adverse effect. | |||
1-FCV-65-8 when B-B ACU is - Mechanical (Unit 1 in LOCA) operating for Unit 1 Failure (valve open by Open (ACU A-A - Electrical Valve position If valves None (See Remarks) Valve on Fan A-A operator action) has not operated Failure indication light in 0-FCV-65-28A and discharge side and B-B is the MCR -28B are open, (0-FCV-65-24) closes operating) - Mechanical there will be when ACU A-A is in Failure negative pressure standby and will prevent on ACU A-A by backflow. | |||
suction ACU fan B-B. | |||
Closed (ACU A-A - Electrical Valve position None (See None (See Remarks) Operator will return to has operated and Failure indication light in Remarks) using ACU A-A. | |||
is on stand-by and the MCR B-B is operating) - Mechanical An additional flow path is Failure available by opening 1-FCV-65-10, 0-FCV-65-28A and 0-FCV-65-28B. | |||
Instrumentation Requirements WBNP-112 | |||
the | Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System Instrumentation Requirements WATTS BAR (Page 3 of 17) | ||
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS 4a. B train isolation Provide decay heat Open (ACU A-A is - Electrical Valve position Parallel flow path to None (See Remarks) Additional flow path is valves at EGTS removal cooling flow in operation) Failure indication light in the ACU A-A is open available which causes no Train A suction path for A-A ACU MCR adverse effect. | |||
2-FCV-65-7 when B-B ACU is - Mechanical (Unit 2 in LOCA) operating for Unit 2 Failure (valve opened by operator action) | |||
Open (ACU A-A - Electrical Valve position If valves None (See Remarks) Valve on Fan A-A has not operated Failure indication light in 0-FCV-65-28A and discharge side and B-B is the MCR -28B are open, (0-FCV-65-24) closes operating) - Mechanical there will be when ACU A-A is in Failure negative pressure standby and will prevent on ACU A-A by backflow. | |||
suction ACU fan B-B. | |||
Closed (ACU A-A - Electrical Valve position None (See None (See Remarks) Operator will return to has operated and Failure indication light in Remarks) using ACU A-A. | |||
is on stand-by and the MCR B-B is operating) - Mechanical An additional flow path is Failure available by opening 2-FCV-65-9, 0-FCV-65-28A and 0-FCV-65-28B. | |||
6.2.3-29 WBNP-112 | |||
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System 6.2.3-30 WATTS BAR (Page 4 of 17) | |||
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS | |||
: 5. A train isolation Provide decay heat Open (ACU B-B is - Electrical Valve position Parallel flow path to None (See Remarks) Additional flow path is valves at EGTS removal cooling path in operation) failure indication light in the ACU B-B is open available which causes no Train B suction for B-B ACU when A-A MCR adverse effect. | |||
1-FCV-65-51 ACU is operating for - Mechanical (Unit 1 in LOCA) Unit 1 (valve opened failure by operator action) | |||
Open (ACU B-B - Electrical Valve position If valves None (See Remarks) Valve on Fan B-B has not operated failure indication light in 0-FCV-65-47A and discharge side and A-A is the MCR - 47B are open, 0-FCV-65-43 closes operating) - Mechanical there will be when ACU B-B is in failure negative pressure standby and will prevent on ACU B-B by backflow. | |||
suction ACU fan A-A. | |||
Closed (ACU B-B - Electrical Valve position None (See None (See Remarks) Operator will return to has operated and failure indication light in Remarks) using ACU B-B. | |||
is on Stand-by the MCR and A-A is - Mechanical An additional flow path is operating) failure available by opening 1-FCV-65-30, 0-FCV-65-47A and 0-FCV-65-47B. | |||
Instrumentation Requirements WBNP-112 | |||
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System Instrumentation Requirements WATTS BAR (Page 5 of 17) | |||
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS 5a. A train isolation Provide decay heat Open (ACU B-B is - Electrical Valve position Parallel flow path to None (See Remarks) Additional flow path is valves at EGTS removal cooling path in operation) failure indication light in the ACU B-B is open available which causes no Train B suction for B-B ACU when A-A MCR adverse effect. | |||
2-FCV-65-50 ACU is operating for - Mechanical (Unit 2 in LOCA) Unit 2 (valve opened failure by operator action) | |||
Open (ACU B-B - Electrical Valve position If valves None (See Remarks) Valve on Fan B-B has not operated failure indication light in 0-FCV-65-47A and discharge side and A-A is the MCR - 47B are open, 0-FCV-65-43 closes operating) - Mechanical there will be when ACU B-B is in failure negative pressure standby and will prevent on ACU B-B by backflow. | |||
suction ACU fan A-A. | |||
Closed (ACU B-B - Electrical Valve position None (See None (See Remarks) Operator will return to has operated and failure indication light in Remarks) using ACU B-B. | |||
is on Stand-by the MCR and A-A is - Mechanical An additional flow path is operating) failure available by opening 2-FCV-65-29, 0-FCV-65-47A and 0-FCV-65-47B. | |||
6.2.3-31 WBNP-112 | |||
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System 6.2.3-32 WATTS BAR (Page 6 of 17) | |||
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS | |||
: 6. Isolation valve at Isolation control valve Closed (ACU A-A - Electrical Low flow alarm and Momentary decrease None (See Remarks) Redundant ACU Fan B-B EGTS Train A that opens on a is in operation) failure valve position in flow starts on low flow signal suction, containment isolation indication light in the from Fan A-A and 1-FCV-65-10 signal so that the - Mechanical MCR Valve 1-FCV-65-30 is (Unit 1 in LOCA) EGTS can exhaust air failure opened. The fan starting from the annulus. It signal is independent of also isolates Train A valve failure. | |||
ACU during normal plant operation. | |||
Closed (both - Electrical Low flow alarm and Momentary None (See Remarks) Train B ACU continues to Trains A-A and failure valve indication light decrease in flow operate with Valve B-B ACUs are in the MCR 1-FCV-65-30 open. | |||
operating) - Mechanical failure Open (Train B-B is - Electrical Valve position Open backflow path None (See Remarks) Flow Control Valve operating. A-A is failure indication light in to ACU A-A 0-FCV-65-24 and not operating and the MCR Backdraft Damper has never - Mechanical 0-65-524 close when operated or has failure ACU A-A is in standby operated and and will prevent stopped.) backflow. | |||
Instrumentation Requirements WBNP-112 | |||
the | Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System Instrumentation Requirements WATTS BAR (Page 7 of 17) | ||
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS 6a. Isolation valve at Isolation control valve Closed (ACU A-A - Electrical Low flow alarm and Momentary decrease None (See Remarks) Redundant ACU Fan B-B EGTS Train A that opens on a is in operation) failure valve position in flow starts on low flow signal suction, containment isolation indication light in the from Fan A-A and 2-FCV-65-9 signal so that the - Mechanical MCR Valve 2-FCV-65-29 is (Unit 2 in LOCA) EGTS can exhaust air failure opened. The fan starting from the annulus. It signal is independent of also isolates Train A valve failure. | |||
ACU during normal plant operation. | |||
Closed (both - Electrical Low flow alarm and Momentary None (See Remarks) Train B ACU continues to Trains A-A and failure valve position decrease in flow operate with Valve B-B ACUs are indication light in 2-FCV-65-29 open. | |||
operating) - Mechanical the MCR failure Open (Train B-B is - Electrical Valve position Open backflow path None (See Remarks) Flow Control Valve operating. A-A is failure indication light in to ACU A-A 0-FCV-65-24 and not operating and the MCR Backdraft Damper has never - Mechanical 0-65-523 close when operated or has failure ACU A-A is in standby operated and and will prevent stopped.) backflow. | |||
6.2.3-33 WBNP-112 | |||
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System 6.2.3-34 WATTS BAR (Page 8 of 17) | |||
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS | |||
: 7. Isolation valves at Isolation control valve Closed (ACU B-B -Electrical failure Low flow alarm and Momentary decrease None (See remarks) Redundant ACU Fan A-A EGTS Train B that opens on a is in operation) valve position in flow starts on low flow signal suction, containment isolation - Mechanical indication light in the from Fan B-B and Valve 1-FCV-65-30 signal so that the failure MCR 1-FCV-65-10 is opened. | |||
(Unit 1 in LOCA) EGTS can exhaust air The fan starting signal is from the annulus. It independent of valve also isolates Train B failure. | |||
ACU during normal plant operation. | |||
Closed (both - Electrical Low flow alarm and Momentary None (See remarks) Train A ACU continues to Trains A-A and failure valve position decrease in flow operate with Valve B-B ACUs are indication light in 1-FCV-65-10 open. | |||
operating.) - Mechanical the MCR failure Open (Train A-A is - Electrical Valve position Open backflow path None (See remarks) Flow Control Valve operating. B-B is failure indication light in to ACU B-B 0-FCV-65-43 and not operating and the MCR backdraft damper has never - Mechanical 0-65-526 close when operated or has failure ACU B-B is in standby operated and and will prevent stopped.) backflow. Also, the additional flow paths will not cause an adverse effect. | |||
Instrumentation Requirements WBNP-112 | |||
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System Instrumentation Requirements WATTS BAR (Page 9 of 17) | |||
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS 7a. Isolation valves at Isolation control valve Closed (ACU B-B - Electrical Low flow alarm and Momentary decrease None (See remarks) Redundant ACU Fan A-A EGTS Train B that opens on a is in operation) failure valve position in flow starts on low flow signal suction, containment isolation indication light in the from Fan B-B and Valve 2-FCV-65-29 signal so that the - Mechanical MCR 2-FCV-65-9 is opened. | |||
(Unit 2 in LOCA) EGTS can exhaust air failure The fan starting signal is from the annulus. It independent of valve also isolates Train B failure. | |||
ACU during normal plant operation. | |||
Closed (both - Electrical Low flow alarm and Momentary None (See remarks) Train A ACU continues to Trains A-A and failure valve position decrease in flow operate with Valve B-B ACUs are indication light in 2-FCV-65-9 open. | |||
operating.) - Mechanical the MCR failure Open (Train B-B is - Electrical Valve position Open backflow path None (See remarks) Flow Control Valve operating. A-A is failure indication light in to ACU A-A 0-FCV-65-24 and not operating and the MCR backdraft damper has never - Mechanical 0-65-525 close when operated or has failure ACU B-B is in standby operated and and will prevent stopped.) backflow. Also, the additional flow paths will not cause an adverse effect. | |||
: 8. EGTS fan Isolates EGTS fan One damper fails - Electrical Low flow alarm and Loss of flow through None (See remarks) Redundant fan starts on discharge isolation from duct distribution closed (EGTS fan failure valve position the affected EGTS low flow signal from the valves system when EGTS is operating) indication light in the train affected train. Fan 0-FCV-65-24 fan is on standby - Mechanical MCR starting signal is 0-FCV-65-43 failure independent of valve failure. | |||
6.2.3-35 WBNP-112 | |||
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System 6.2.3-36 WATTS BAR (Page 10 of 17) | |||
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS | |||
: 9. Shield building Open air path for One damper fails - Electrical Damper position None (See Remarks) None (See Remarks) Damper in parallel flow exhaust isolation EGTS exhaust to be closed failure indication light in the path is open. | |||
dampers discharged to either MCR 1-FCO-65-26 shield building vent - Mechanical 1-FCO-65-27 and recirculated air failure 2-FCO-65-45 flow to either annulus 2-FCO-65-46 10 EGTS inlet flow elements abandoned in place (1-FE-65-54 and 2-FE-65-3). | |||
11 Shield building Exhaust flow elements abandoned in place (1-FE-65-84 and -85, 1-FE-65-78, 2-FE-65-84 and -85, 2-FE-65-78) | |||
Instrumentation Requirements WBNP-112 | |||
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System Instrumentation Requirements WATTS BAR (Page 11 of 17) | |||
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS | |||
- | : 12. Back draft Prevent backflow Damper closed - Mechanical Low flow alarm Momentary decrease None (See Remarks) Redundant ACU Fan B-B dampers through Train A ACU (Train A ACU is in failure indication light in the in flow from annulus starts on low flow from 0-65-523 when Train B ACU is in operation and MCR Train A-A. Fan starting 0-65-524 operation Train B ACU is in signal is independent of standby) damper failure. | ||
- | Damper closed - Mechanical Low flow alarm None (See None (See Remarks) Train B ACU continues to (Both Train A & failure indication light in Remarks) operate and Train A will Train B are the MCR be turned off by operator. | ||
operational) | |||
: 13. Back draft Prevent backflow Damper closed - Mechanical Low flow alarm Momentary decrease None (See Remarks) Redundant ACU Fan A-A dampers through Train B ACU (Train B ACU is in failure indication light in the in flow from annulus starts on low flow from 0-65-525 when Train A ACU is in operation and MCR Train B-B. Fan starting 0-65-526 operation Train A ACU is in signal is independent of standby) damper failure. | |||
Damper closed - Mechanical Low flow alarm None (See None (See Remarks) Train A ACU continues to (Both Train A & failure indication light in Remarks) operate and Train B will Train B are the MCR be turned off by operator. | |||
operational) 6.2.3-37 WBNP-112 | |||
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System 6.2.3-38 WATTS BAR (Page 12 of 17) | |||
-2.1 | METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS | ||
-P. However, the worst case PCO failure has been analyzed to exist with both trains of EGTS fans running for the first one to two hours after event initiation; and then one fan running thereafter due to operator action to shut off one EGTS fan. | : 14. Modulating Modulates EGTS flow Damper closed, - Mechanical Pressure differential With the worst case None. The elevated Off-site and control room dampers released to outside open or improper linkage failure is indicated in the PCO single failure, 957 cfm (832 cfm for radiological dose 1-PCO-65-80 atmosphere, modulation.The MCR to detect the the EGTS maintains U2) short term / 694 analyses demonstrate 1-PCO-65-82 controlling to the worst case PCO - Control Loop -2.1 (-1.88 for U2) annulus -P at -2.1 (- cfm (604 cfm for U2) that the offsite and 1-PCO-65-88 required annulus single failure is Failure of one w.g. annulus 1.88 for U2) w.g. long term EGTS control room dose results 1-PCO-65-89 negative pressure such that either Train of PCOs. -P. However, the (steady state) during exhaust flow associate remain below the 2-PCO-65-80 1(2)-PCO-65-80 worst case PCO the short term, which with the worst case regulatory limits, when 2-PCO-65-82 or -82 fail open to failure has been is acceptable since it PCO single failure the elevated EGTS 2-PCO-65-88 the shield building analyzed to exist is more negative than mode is addressed in exhaust flows associated 2-PCO-65-89 stack, and the with both trains of the Remarks. with the worst case PCO opposite train EGTS fans running -1.45 w.g. controller single failure scenario are PCOs still for the first one to setpoint. When one considered. | ||
modulate and two hours after EGTS fan is stopped attempt to event initiation; and between one and two maintain annulus - then one fan running hours by operator P at the thereafter due to action, the resulting | |||
-1.45 w.g. control operator action to configuration setpoint. This shut off one EGTS maintains annulus single failure fan. -P at -1.60 (-1.48 scenario takes the for U2) w.g., which is short term annulus still slightly more steady state -P to negative than | |||
-2.1 (-1.88 for -1.45 w.g. | |||
U2) w.g. | |||
(i.e., failed PCO train with open flow path to the shield building stack and Instrumentation Requirements non-failed PCO train with open recirculation flow path to the annulus and two fans operating.) | |||
WBNP-112 | |||
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System Instrumentation Requirements WATTS BAR (Page 13 of 17) | |||
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS | |||
: 15. Isolation valves Isolates EGTS One valve closed - Electrical Valve position One of the two None (See Remarks) Redundant flow path is 1-PCV-65-81 ductwork from outside when EGTS is in failure indication light in the parallel flow paths is available 1-PCV-65-83 atmosphere and ring operation MCR lost 1-PCV-65-86 header during normal - Mechanical 1-PCV-65-87 plant operation Failure 2-PCV-65-81 2-PCV-65-83 2-PCV-65-86 2-PCV-65-87 | |||
: 16. Isolation valves Valves open to remove One valve opens -Electrical failure Valve position None (See Remarks) None (See Remarks) Redundant isolation 0-FCV-65-28A decay heat in the idle when bypass indication light in the valves 0-FCV-65-28B train ACU cooling is not in - Mechanical MCR operation Failure One valve closed - Electrical Valve position None (See Remark) None (See Remarks) Bypass cooling provision when bypass failure indication light in will not be used unless cooling is in the MCR ACU fails and enough operation - Mechanical heat is generated by failure radioactivity collected on HEPA and charcoal adsorber to raise the charcoal bed temperature significantly. | |||
Therefore, a second failure (closed isolation valve) need not be postulated. | |||
6.2.3-39 WBNP-112 | |||
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System 6.2.3-40 WATTS BAR (Page 14 of 17) | |||
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS | |||
: 17. Isolation valves Valves open to remove One valve opens - Electrical Valve position None (See Remarks) None (See Remarks) Redundant isolation 0-FCV-65-47A decay heat in the idle when bypass failure indication light in the valves 0-FCV-65-47B train ACU cooling is not in MCR operation - Mechanical failure One valve closed - Electrical Valve position None (See Remarks) None (See Remarks) Bypass cooling provision when bypass failure indication light in will not be used unless cooling is in the MCR ACU fails and enough operation - Mechanical heat is generated by failure radioactivity collected on HEPA and charcoal adsorber to raise the charcoal bed temperature significantly. | |||
Therefore, a second failure (closed isolation valve) need not be postulated. | |||
: 18. Flow elements Opens decay heat No signal sent - Electrical Valve position None (See Remarks) None (See Remarks) Bypass cooling provision 0-FS-65-31A/B removal isolation failure indication light in the will not be used unless 0-FS-65-55A/B valves to the operating MCR ACU fails and enough ACU when no flow is heat is generated by sensed at the idle ACU radioactivity collected on HEPA and charcoal adsorber to raise the charcoal bed temperature Instrumentation Requirements significantly. Therefore, a second failure (closed isolation valve) need not be postulated. | |||
WBNP-112 | |||
cooling is | Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System Instrumentation Requirements WATTS BAR (Page 15 of 17) | ||
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS | |||
: 19. Flow elements Starts EGTS standby No signal sent - Electrical Valve position Momentary decrease None (See Remarks) Bypass cooling provision 0-FS-65-31B/A ACU unit upon loss of failure indication light in the in flow from annulus will not be used unless 0-FS-65-55B/A flow in normally MCR ACU fails and enough operating ACU heat is generated by radioactivity collected on HEPA and charcoal adsorber to raise the charcoal bed temperature significantly. | |||
Therefore, a second failure (closed isolation valve because signal not sent) need not be postulated. | |||
: 20. Flow elements Shuts off relative No signal sent - Electrical Low flow and high Humidity heater may None (See Remarks) The EGTS fan can be 0-FS-65-25A/B humidity heater on low failure temperature alarms stay on after EGTS stopped either by 0-FS-65-44A/B air flow and alarm in in the MCR fan stops operators action or fan the MCR failure, which is a single failure; the other EGTS fan is available to function. The heater requires two signals to operate: one from flow switch and one from temperature switch. | |||
Therefore, heater not receiving the signal need not be assumed. | |||
6.2.3-41 WBNP-112 | |||
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System 6.2.3-42 WATTS BAR (Page 16 of 17) | |||
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS | |||
: 21. Flow elements Opens decay heat No signal sent - Electrical Valve position None (See Remarks) None (See Remarks) Bypass cooling provision 0-FS-65-25B/A removal isolation failure indication light in the will not be used unless 0-FS-65-44B/A valves on idle ACU MCR ACU fails and enough when high flow is heat is generated by sensed at the radioactivity collected on operating ACU HEPA and charcoal adsorber to raise the charcoal bed temperature significantly. | |||
Therefore, a second failure (closed isolation valve because signal not sent) need not be postulated. | |||
22 Train A Provides Class 1E Loss of or Diesel generator Alarm and Loss of redundancy None (See Remarks) Redundant train of EGTS Emergency Power diesel-backed power inadequate failure; bus fault indication in the in EGTS exhaust is turned on by automatic supply to active Voltage (Train A); MCR flow paths and manual actions on components of Train A operator error loss of fan airflow, or of EGTS annulus -P, which ensures that the EGTS safety functions are continued to be performed. | |||
23 Train B Provides Class 1E Loss of or Diesel generator Alarm and Loss of redundancy None (See Remarks) Redundant train of EGTS Emergency Power diesel-backed power inadequate failure; bus fault indication in the in EGTS exhaust is turned on by automatic supply to active Voltage (Train B); MCR flow paths and manual actions on components of Train B operator error loss of fan airflow, or Instrumentation Requirements of EGTS annulus -P, which ensures that the EGTS safety functions are continued to be performed. | |||
WBNP-112 | |||
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System Instrumentation Requirements WATTS BAR (Page 17 of 17) | |||
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS 24 Deluge Valve Floods the carbon Spurious - Electrical Local and MCR None (See None (See Remarks) ACU will not be flooded 0-FCV-26-175 absorbers in the event actuation failure alarms on water Remarks) since the fusible links on of fire discharge the spray heads will be | |||
- Mechanical closed due to absence of failure heat. | |||
24a Deluge System Floods the carbon Spurious - Fusible Link None Loss of redundancy None (See Remarks) Opposite train ACU is Piping/Heads on absorbers in the event actuation Failure in EGTS unaffected and remains Train A of fire available. | |||
- Piping Failure 25 Deluge Valve Floods the carbon Spurious - Electrical Local and MCR None (See None (See Remarks) ACU will not be flooded 0-FCV-26-179 absorbers in the event actuation failure alarms on water Remarks) since the fusible links on of fire discharge the spray heads will be | |||
- Mechanical closed due to absence of failure heat. | |||
25a Deluge System Floods the carbon Spurious - Fusible Link None Loss of redundancy None (See Remarks) Opposite train ACU is Piping/Heads on absorbers in the event actuation Failure in EGTS unaffected and remains Train B of fire available. | |||
- Piping Failure 6.2.3-43 WBNP-112 | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 1 of 27) 6.2.3-44 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 1 Auxiliary Building De-energizes solenoid Signal fails. Train A vital ac bus MCR indication of Loss of None. (See Train A and Train B ABI initiating Isolation (ABI) valves to close failure; Relay VKA1 only one train redundancy in Remarks) signals are derived from signal Train A associated dampers failure; Train A ABGTS fan starting ABSCE isolation independent (train-separated) and establish AB initiating signal and one train of and in ABGTS until qualified devices. | |||
secondary containment (Phase A containment ABSCE dampers operator starts enclosure; stops AB isolation, high rad in closing. Train A ABGTS Either train signal is sufficient to general ventilation refueling area, manually from stop all AB general vent supply fans; starts various high temp. in Aux. MCR, after and exhaust fans and fuel handling ESF room coolers; Building general ascertaining that area exhaust fans. SInce ABSCE starts ABGTS fans to supply duct) failure. Train B ABI signal dampers are arranged in series, maintain negative is not spurious. either trains actuation is adequate pressure in the ABSCE to establish the ABSCE boundary. | |||
and remove contaminants from the ABSCE air prior to discharge to atmosphere. | |||
Starts Train A ABGTS, Same as Same as above. Same as above. Same as above. None. (See Only Train B ABGTS will start and closes Train A ABSCE above. Remarks). only Train B ABSCE isolation isolation dampers, dampers will close. Train A stops Train A containment purge air supply fan containment purge air and exhaust fan may be running, supply and exhaust and the Incore Instrument Room fans (Ref.5.28) suppy and exhaust fans will stop (both Train B). For conservatism, it is assumed that all exhaust fans are stopped. Preoperational and surveillance tests have shown that, in this configuration, the ABGTS is able to fulfill its safety functions. | |||
Same as above. Spuriously Operator error, MCR indicating *Disrupts the None. (See Unnecessary isolation of ABSCE starts. spurious initiating lights on ABGTS normally operating Remarks) and actuation of ABGTS, as well Instrumentation Requirements signal (initiating signals start and ABSCE ventilation system, as disrupting the normally listed above) dampers closure. and starts safety- operating ventilation systems and related systems starting the ESF pump room and and components. area coolers. | |||
*Interim U1 configuration: As a result of the changes made by DCN 56414, a spurious ABI signal would also result in a Containment Vent Isolation (CVI) signal. | |||
WBNP-112 Dual Unit configuration: EDCR 55801 provides for a functional cross-tie between the two units which would cause a refueling unit CVI upon spurious ABI signal. | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 2 of 27) | |||
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 2 Auxiliary Building De-energizes solenoid Signal fails. Train B vital ac bus MCR indication of Loss of None (See Train A and Train B ABI initiating Isolation (ABI) valves to close failure; Relay VKA1 only one train redundancy in Remarks) signals are derived from signal Train B associated dampers failure; Train B ABGTS fan starting ABSCE isolation independent (train-separated) and establish AB initiating signal (Phase and one train of and in ABGTS until qualified devices. | |||
secondary containment A containment ABSCE dampers operator starts enclosure; stops AB isolation, high rad in closing. Train B ABGTS Either train signal is sufficient to general ventilation refueling area, high manually from stop all AB general vent supply fans; starts various temp. in Aux. Building MCR, after and exhaust fans and fuel handling ESF room coolers; general supply duct) ascertaining that area exhaust fans. SInce ABSCE starts ABGTS fans to failure. Train A ABI signal dampers are arranged in series, maintain negative is not spurious either trains actuation is adequate pressure in ABSCE and to establish the ABSCE boundary. | |||
remove contaminants from the ABSCE air prior to discharge to atmosphere. | |||
Starts Train B ABGTS, Same as Same as above. Same as above. Same as above. None. (See Only Train B ABGTS will start and closes Train B ABSCE above. Remarks). only Train B ABSCE isolation isolation dampers, dampers will close. Train B stops Train B containment purge air supply fan containment purge air and exhaust fan may be running, supply and exhaust and the Incore Instrument Room fans and stops the suppy and exhaust fans may be Incore Instrument running. For conservatism, it is Room supply and assumed that all exhaust fans are exhaust fans (Ref.5.28) stopped. Preoperational and surveillance tests have shown that, in this configuration, the ABGTS is able to fulfill its safety functions. | |||
(See Section 8.3 for detail). | |||
Same as above. Spuriously Operator error, MCR indicating *Disrupts the None. (See Unnecessary isolation of ABSCE starts. spurious initiating lights on ABGTS normally operating Remarks). and actuation of ABGTS, as well signal (initiating signals start and ABSCE ventilation systems as disrupting the normally listed above) dampers closure. and starts safety- operating ventilation systems and related systems starting the ESF pump room and and components area coolers. | |||
WBNP-112 | |||
*Interim U1 configuration: As a result of the changes made by DCN 56414, a spurious ABI signal would also result in a Containment Vent Isolation (CVI) signal. | |||
Dual Unit configuration: EDCR 55801 provides for a functional cross-tie between the two units which would cause a refueling unit CVI upon spurious ABI signal. | |||
6.2.3-45 | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 3 of 27) 6.2.3-46 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 3 ABGTS Exhaust Draws a portion of air in Fails to start or Mechanical failure; Indicating light in Loss of None. Handswitches for ABGTS Fans Fan A-A the ABSCE through an fails to run. Train A power failure; the MCR. redundancy in ABGTS Fan A-A and B-B in the MCR should air cleanup unit (ACU) Train A ABI signal ABGTS. B-B can normally be in the A-Auto position. | |||
to remove radioactive (HS in A-Auto). perform the On an ABI signal, both fans start contaminants and functions of and the operator may stop one fan discharge into the maintaining and place its handswitch in the shield building exhaust the ABSCE at P-Auto (pull-out) position. This vent to maintain a a negative mode of operation is expected to negative pressure in pressure and occur after 30 minutes of two fan the ABSCE relative to removing operation. During an ABI, the fan the outside. contaminants. in the P-Auto mode will start automatically on insufficient negative pressure in the ABSCE relative to the outside. An alarm is provided for the condition when flow is inadequate 45 seconds after fan start. | |||
Starts Spurious Train A ABI See "Remarks" Vacuum relief line None (See Ind. light in the MCR provides spuriously. signal (HS in A-Auto); column. dampers may open Remarks) indication to operator that fan is spurious low flow to prevent running. However, if only one signal from Fan B-B excessive negative ABGTS train starts when both fans after valid ABI signal pressure in ABSCE are in A-Auto or if the fan in P-Auto (HS in P-Auto). by admitting starts, the operator cannot outside air. determine whether the signal is valid or spurious (no detection of spurious operation). This is acceptable since there is no impact on plant safety without a second failure (e.g., failure of a vacuum relief damper). | |||
Instrumentation Requirements See end of Table 6.2.3-3 for the effects of the potential ABGTS fan failures on the EGTSs ability to maintain the annulus -P more negative than that of the ABSCE. | |||
WBNP-112 | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 4 of 27) | |||
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 4 ABGTS Exhaust Draws a portion of air in Fails to start or Mechanical failure; Indicating light in Loss of None. Handswitches for ABGTS Fans Fan B-B the ABSCE through an fails to run. Train B power failure; the MCR. redundancy in ABGTS Fan A-A and B-B, in the MCR should air cleanup unit (ACU) Train B ABI signal ABGTS. A-A can normally be in the A-Auto position. | |||
to remove radioactive failure (HS in A-Auto). perform the On an ABI signal, both fans start contaminants and functions of and the operator may stop one fan discharge into the maintaining and place its handswitch in the shield building exhaust the ABSCE at P-Auto (pull-out) position. This vent to maintain a a negative mode of operation is expected to negative pressure in pressure and occur after 30 minutes of two fan the ABSCE relative to removing operation. During an ABI, the fan the outside. contaminants. in the P-Auto mode will start automatically on insufficient negative pressure in the ABSCE relative to the outside. An alarm is provided for the condition when flow is inadequate 45 seconds after fan start. | |||
Starts Spurious Train B ABI See "Remarks" Vacuum relief line None. Ind. light in the MCR provides spuriously. signal (HS in A-Auto); column. dampers may open indication to operator that fan is spurious low flow to prevent running. However, if only one signal from Fan A-A excessive negative ABGTS train starts when both fans after valid ABI signal pressure in ABSCE are in A-Auto or if the fan in P-Auto (HS in P-Auto). by admitting starts, the operator cannot outside air. determine whether the signal is valid or spurious (no detection of spurious operation). This is acceptable since there is no impact on plant safety without a second failure (e.g., failure of a vacuum relief damper). | |||
See end of Table 6.2.3-3 for the effects of the potential ABGTS fan failures on the EGTSs ability to maintain the annulus -P more negative than that of the ABSCE. | |||
6.2.3-47 WBNP-112 | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 5 of 27) 6.2.3-48 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 5 ABGTS Fan A-A Provides flowpath for Fails to open Mechanical failure. Alarm in the MCR Loss of None (See ABGTS Fan A-A Inlet and Outlet Inlet Damper ABGTS Exhaust Fan or stuck from 1-FS-30-146 redundancy in Remarks) Dampers 1-FCO-30-146A and 1-FCO-30-146B A-A. closed. ABGTS. 1-FCO-30-146B open on starting of associated fan and close when the fan stops. | |||
ABGTS fan B-B provides redundancy. | |||
Provides isolation of Fails to close Mechanical failure Alarm in the MCR None (See None (See Damper 146A provides ACU A-A when fan A-A or stuck open. from 1-FS-30-146 Remarks) Remarks) redundancy (both dampers fail is not running. closed). | |||
6 ABGTS Fan A-A Provides flowpath for Fails to open Mechanical failure. Alarm in the MCR Loss of None (See ABGTS Fan A-A Inlet and Outlet Outlet Damper ABGTS Exhaust Fan or stuck from 1-FS-30-146 redundancy in Remarks) Dampers 1-FCO-30-146A and 1-FCO-30-146A A-A. closed. ABGTS. 1-FCO-30-146B open on starting of associated fan and close when the fan stops. | |||
Provides isolation of Fails to close Mechanical failure. Alarm in the MCR None (See None (See Damper 146B provides ACU A-A when fan A-A or stuck open. from 1-FS-30-146 Remarks) Remarks) redundancy (both dampers fail is not running. closed). | |||
7 ABGTS Fan B-B Provides flowpath for Fails to open Mechanical failure. Alarm in the MCR Loss of None (See ABGTS Fan B-B Inlet and Outlet Inlet Damper ABGTS Exhaust Fan or stuck from 2-FS-30-165 redundancy in Remarks) Dampers 2-FCO-30-157A and 2-FCO-30-157B B-B. closed. ABGTS. 2-FCO-30-157B open on starting of associated fan and close when the fan stops. | |||
ABGTS fan A-A provides redundancy. | |||
Instrumentation Requirements Provides isolation of Fails to close Mechanical failure. Alarm in the MCR Loss of None (See Damper 157A provides ACU B-B when fan B-B or stuck open from 2-FS-30-165 redundancy in Remarks) redundancy (both dampers fail is not running. ABGTS. closed). | |||
WBNP-112 | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 6 of 27) | |||
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 8 ABGTS Fan B-B Provides flowpath for Fails to open Mechanical failure. Alarm in the MCR Loss of None (See ABGTS Fan B-B Inlet and Outlet Outlet Damper ABGTS Exhaust Fan or stuck from 2-FS-30-165 redundancy in Remarks) Dampers 2-FCO-30-157A and 2-FCO-30-146A B-B. closed. ABGTS. 2-FCO-30-157B open on starting of associated fan and close when the fan stops. | |||
ABGTS fan A-A provides redundancy. | |||
Provides isolation of Fails to close Mechanical failure. Alarm in the MCR Loss of None (See Damper 157B provides ACU B-B when fan B-B or stuck open from 2-FS-30-165 redundancy in Remarks) redundancy (both dampers fail is not running. ABGTS. closed). | |||
9 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-30-137 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A (0-Train A signal to isolate Fuel or spuriously Train A ABI or high rad isolation of Fuel Damper FCO-30-137) and Train B (0-FCO-Handling Area Exhaust opens. in refueling area signal Handling Area 0-FCO-30-138 30-138) dampers, in series, are Fan A-A and to failure; HS failure to Exhaust Fan A-A. provides provided with non-safety control establish boundary for spring return from isolation and air. Loss of the non-safety related ABGTS. open to A-Auto. maintains the control air does not prevent the ABSCE. damper from closing. | |||
Independence of Train A and Train B isolation signals is discussed in "Remarks" under items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
6.2.3-49 WBNP-112 | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 7 of 27) 6.2.3-50 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 10 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-30-138 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A (0-Train B signal to isolate Fuel or spuriously Train B ABI or high rad isolation of Fuel Damper FCO-30-137) and Train B (0-FCO-Handling Area Exhaust opens. in refueling area signal Handling Area 0-FCO-30-137 30-138) dampers, in series, are Fan A-A and to failure; HS failure to Exhaust Fan A-A. provides provided with non-safety control establish boundary for spring return from isolation and air. Loss of the non-safety related ABGTS. open to A-Auto. maintains the control air does not prevent the ABSCE. damper from closing. | |||
Independence of Train A and Train B isolation signals is discussed in "Remarks" under items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
11 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-30-140 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A (0-Train A signal to isolate Fuel or spuriously Train A ABI or high rad isolation of Fuel Damper FCO-30-140) and Train B (0-FCO-Handling Area Exhaust opens. in refueling area signal Handling Area 0-FCO-30-141 30-141) dampers, in series, are Fan B-B and to failure; HS failure to Exhaust Fan B-B. provides provided with non-safety control establish boundary for spring return from isolation and air. Loss of the non-safety related ABGTS. open to A-Auto. maintains the control air does not prevent the ABSCE. damper from closing. | |||
Independence of Train A and Train B, isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | |||
Damper failure to open is not listed Instrumentation Requirements since the damper has no safety function to open for DBE mitigation. | |||
WBNP-112 | |||
and | Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 8 of 27) | ||
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 12 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-30-141 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train A 125 Vdc power. Train A (0-Train B signal to isolate Fuel or spuriously Train B ABI or high rad isolation of Fuel Damper FCO-30-140) and Train B (0-FCO-Handling Area Exhaust opens. in refueling area signal Handling Area 0-FCO-30-140 30-141) dampers, in series, are Fan B-B and to failure; HS failure to Exhaust Fan B-B. provides provided with non-safety control establish boundary for spring return from isolation and air. Loss of the non-safety related ABGTS. open to A-Auto. maintains the control air does not prevent the ABSCE. damper from closing. | |||
Independence of Train A and Train B, isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
13 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 2-FCO-30-21 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate AB or spuriously Train A ABI or high rad isolation of part of Damper (2-FCO-30-21) and Train B Gen Supply Fans 2A-A opens. in refueling area signal ductwork on Unit 2 2-FCO-30-22 (2-FCO-30-22) dampers, in series, and 2B-B and to failure; HS failure to side of AB. provides are provided with non-safety establish boundary for spring return from isolation and control air and both dampers fail ABGTS. open to A-Auto. maintains the closed on loss of control air. | |||
ABSCE. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
6.2.3-51 WBNP-112 | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 9 of 27) 6.2.3-52 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 14 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 2-FCO-30-22 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate AB or spuriously Train B ABI or high rad isolation of part of Damper (2-FCO-30-21) and Train B Gen Supply Fans 2A-A opens. in refueling area signal ductwork on Unit 2 2-FCO-30-21 (2-FCO-30-22) dampers, in series, and 2B-B and to failure; HS failure to side of AB. provides are provided with non-safety establish boundary for spring return from isolation and control air and both dampers fail ABGTS. open to A-Auto. maintains the closed on loss of control air. | |||
ABSCE. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
15 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1-FCO-30-86 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate AB or spuriously Train A ABI or high rad isolation of part of Damper (1-FCO-30-86) and Train B Gen Supply Fans 1A-A opens. in refueling area signal ductwork on Unit 1 1-FCO-30-87 (1-FCO-30-87) dampers, in series, and 1B-B and to failure; HS failure to side of AB. provides are provided with non-safety establish boundary for spring return from isolation and control air and both dampers fail ABGTS. open to A-Auto. maintains the closed on loss of control air. | |||
ABSCE. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE Instrumentation Requirements mitigation. | |||
WBNP-112 | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 10 of 27) | |||
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 16 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1-FCO-30-87 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate AB or spuriously Train B ABI or high rad isolation of part of Damper (1-FCO-30-86) and Train B Gen Supply Fans 1A-A opens. in refueling area signal ductwork on Unit 1 1-FCO-30-86 (1-FCO-30-87) dampers, in series, and 1B-B and to failure; HS failure to side of AB. provides are provided with non-safety establish boundary for spring return from isolation and control air and both dampers fail ABGTS. open to A-Auto. maintains the closed on loss of control air. | |||
ABSCE. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
17 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1-FCO-30-106 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate AB or spuriously Train A ABI or high rad isolation of part of Damper (1-FCO-30-106) and Train B Gen Supply Fans 1A-A opens. in refueling area signal ductwork on Unit 1 1-FCO-30-107 (1-FCO-30-107) dampers, in and 1B-B and to failure; HS failure to side of AB. provides series, are provided with establish boundary for spring return from isolation and non-safety control air and both ABGTS. open to A-Auto. maintains the dampers fail closed on loss of ABSCE. control air. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
6.2.3-53 WBNP-112 | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 11 of 27) 6.2.3-54 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 18 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1-FCO-30-107 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate AB or spuriously Train B ABI or high rad isolation of part of Damper (1-FCO-30-106) and Train B Gen Supply Fans 1A-A opens. in refueling area signal ductwork on Unit 1 1-FCO-30-106 (1-FCO-30-107) dampers, in and 1B-B and to failure; HS failure to side of AB. provides series, are provided with establish boundary for spring return from isolation and non-safety control air and both ABGTS. open to A-Auto. maintains the dampers fail closed on loss of ABSCE. control air. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
19 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 2-FCO-30-108 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate AB or spuriously Train A ABI or high rad isolation of part of Damper (2-FCO-30-108) and Train B Gen Supply Fans 2A-A opens. in refueling area signal ductwork on Unit 2 2-FCO-30-109 (2-FCO-30-109) dampers, in and 2B-B and to failure; HS failure to side of AB. provides series, are provided with establish boundary for spring return from isolation and non-safety control air and both ABGTS. open to A-Auto. maintains the dampers fail closed on loss of ABSCE. control air. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE Instrumentation Requirements mitigation. | |||
WBNP-112 | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 12 of 27) | |||
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 20 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 2-FCO-30-109 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate AB or spuriously Train B ABI or high rad isolation of part of Damper (2-FCO-30-108) and Train B Gen Supply Fans 2A-A opens. in refueling area signal ductwork on Unit 2 2-FCO-30-108 (2-FCO-30-109) dampers, in and 2B-B and to failure; HS failure to side of AB. provides series, are provided with establish boundary for spring return from isolation and non-safety control air and both ABGTS. open to A-Auto. maintains the dampers fail closed on loss of ABSCE. control air. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
21 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1-FCO-30-160 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate AB or spuriously Train A ABI or high rad isolation of AB Gen Damper (1-FCO-30-160) and Train B Gen Exhaust Fan 1A-A opens. in refueling area signal Exhaust Fan 1A-A. 1-FCO-30-161 (1-FCO-30-161) dampers, in suction and to establish failure; HS failure to provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air. Loss of the open to A-Auto. maintains the non-safety related control air does ABSCE. not prevent the damper from closing. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
6.2.3-55 WBNP-112 | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 13 of 27) 6.2.3-56 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 22 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1-FCO-30-161 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train B Train B signal to isolate AB or spuriously Train B ABI or high rad isolation of AB Gen Damper (1-FCO-30-160) and Train B Gen Exhaust Fan 1A-A opens. in refueling area signal Exhaust Fan 1A-A. 1-FCO-30-160 (1-FCO-30-161) dampers, in suction and to establish failure; HS failure to provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air. Loss of the open to A-Auto. maintains the non-safety related control air does ABSCE. not prevent the damper from closing. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
23 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1-FCO-30-166 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate AB or spuriously Train A ABI or high rad isolation of AB Gen Damper (1-FCO-30-166) and Train B Gen Exhaust Fan 1B-B opens. in refueling area signal Exhaust Fan 1B-B. 1-FCO-30-167 (1-FCO-30-167) dampers, in suction and to establish failure; HS failure to provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air. Loss of the open to A-Auto. maintains the non-safety related control air does ABSCE. not prevent the damper from closing. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | |||
Damper failure to open is not listed Instrumentation Requirements since the damper has no safety function to open for DBE mitigation. | |||
WBNP-112 | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 14 of 27) | |||
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 24 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1-FCO-30-167 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate AB or spuriously Train B ABI or high rad isolation of AB Gen Damper (1-FCO-30-166) and Train B Gen Exhaust Fan 1B-B opens. in refueling area signal Exhaust Fan 1B-B. 1-FCO-30-166 (1-FCO-30-167) dampers, in suction and to establish failure; HS failure to provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air. Loss of the open to A-Auto. maintains the non-safety related control air does ABSCE. not prevent the damper from closing. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
- | 25 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 2-FCO-30-271 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate AB or spuriously Train A ABI or high rad isolation of AB Gen Damper (2-FCO-30-271) and Train B Gen Exhaust Fan 2A-A opens. in refueling area signal Exhaust Fan 2A-A. 2-FCO-30-272 (2-FCO-30-272) dampers, in suction and to establish failure; HS failure to provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air. Loss of the open to A-Auto. maintains the non-safety related control air does ABSCE. not prevent the damper from closing. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | ||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
6.2.3-57 WBNP-112 | |||
A-A. | Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 15 of 27) 6.2.3-58 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 26 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 2-FCO-30-272 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate AB or spuriously Train B ABI or high rad isolation of AB Gen Damper (2-FCO-30-271) and Train B Gen Exhaust Fan 2A-A opens. in refueling area signal Exhaust Fan 2A-A. 2-FCO-30-271 (2-FCO-30-272) dampers, in suction and to establish failure; HS failure to provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air. Loss of the open to A-Auto. maintains the non-safety related control air does ABSCE. not prevent the damper from closing. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | ||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
27 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 2-FCO-30-275 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate AB or spuriously Train A ABI or high rad isolation of AB Gen Damper (2-FCV-30-275) and Train B Gen Exhaust Fan 2B-B opens. in refueling area signal Exhaust Fan 2B-B. 2-FCO-30-276 (2-FCV-30-276) dampers, in suction and Exhaust failure; HS failure to provides series, are provided with Fan B-B and to spring return from isolation and non-safety control air. Loss of the establish boundary for open to A-Auto. maintains the non-safety related control air does ABGTS. ABSCE. not prevent the damper from closing. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | |||
Damper failure to open is not listed Instrumentation Requirements since the damper has no safety function to open for DBE mitigation. | |||
WBNP-112 | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 16 of 27) | |||
ITEM | Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 28 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 2-FCO-30-276 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate AB or spuriously Train B ABI or high rad isolation of AB Gen Damper (2-FCV-30-275) and Train B Gen Exhaust Fan 2B-B opens. in refueling area signal Exhaust Fan 2B-B. 2-FCO-30-275 (2-FCV-30-276) dampers, in suction area and to failure; HS failure to provides series, are provided with establish boundary for spring return from isolation and non-safety control air. Loss of the ABGTS. open to A-Auto. maintains the non-safety related control air does ABSCE. not prevent the damper from closing. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | ||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
Independence of Train A and Train B isolation signals is discussed in "Remarks" under | 29 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1,2-FCO-30-294 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A** signal to isolate Purge or spuriously Train A ABI or high rad isolation of Purge Damper 1,2- (1,2-FCV-30-294) and Train B Air Supply Fan inlet opens. in refueling area signal Air Supply Fan inlet FCO-30-295 (1,2-FCV-30-295) dampers, in duct and to establish failure; HS failure to duct. provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air and both open to A-Auto. maintains the dampers fail closed on loss of ABSCE. control air. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | ||
Solenoid circuits for 1,2-FCO-30-294 and 1,2-FCO-30-295 are independent, with trained Class 1E power and trained ABI signal. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE WBNP-112 mitigation. | |||
6.2.3-59 | |||
** Unit 2 component, 2-FCO-30-294, was added for dual unit operation. | |||
ABGTS.Stuck open, fails to close, | Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 17 of 27) 6.2.3-60 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 30 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1,2-FCO-30-295 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B** signal to isolate Purge or spuriously Train B ABI or high rad isolation of Purge Damper 1,2- (1,2-FCV-30-294) and Train B Air Supply Fan inlet opens. in refueling area signal Air Supply Fan inlet FCO-30-294 (1,2-FCV-30-295) dampers, in duct and to establish failure; HS failure to duct. provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air and both open to A-Auto. maintains the dampers fail closed on loss of ABSCE. control air. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | ||
Solenoid circuits for 1,2-FCO-30-294 and 1,2-FCO-30-295 are independent, with trained Class 1E power and trained ABI signal. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
31 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-30-122 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate the or spuriously Train A ABI or high rad isolation of cask Damper (0-FCO-30-122) and Train B cask loading area opens. in refueling area signal loading area 0-FCO-30-123 (0-FCO-30-123) dampers, in exhaust and to failure; HS failure to exhaust. provides series, are provided with establish boundary for spring return from isolation and non-safety control air and both ABGTS. open to A-Auto. maintains the dampers fail closed on loss of Damper re-opens on ABSCE. control air. Independence of Instrumentation Requirements loss (or RESET) of ABI Train A and Train B isolation signal. signals is discussed in "Remarks" under Items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE WBNP-112 mitigation. | |||
** Unit 2 component, 2-FCO-30-294, was added for dual unit operation. | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 18 of 27) | |||
Indicating light in | Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 32 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-30-123 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate the or spuriously Train B ABI or high rad isolation of cask Damper (0-FCO-30-122) and Train B cask loading area opens. in refueling area signal loading area 0-FCO-30-122 (0-FCO-30-123) dampers, in exhaust and to failure; HS failure to exhaust. provides series, are provided with establish boundary for spring return from isolation and non-safety control air and both ABGTS. open to A-Auto. maintains the dampers fail closed on loss of Damper re-opens on ABSCE. control air. Independence of loss (or RESET) of ABI Train A and Train B isolation signal. signals is discussed in "Remarks" under Items 1 and 2 of this table. | ||
Independence of Train A and Train B | Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | ||
33 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Train B Damper fails closed on loss of 0-FCO-30-129 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Damper 0- Train A 125 Vdc power. Train A Train A signal to isolate the or spuriously Train A ABI or high rad isolation of cask FCO-30-130 (0-FCO-30-129) and Train B cask loading area opens. in refueling area signal loading area provides (0-FCO-30-130) dampers, in supply and to establish failure; HS failure to supply. isolation and series, are provided with boundary for ABGTS. spring return from maintains the non-safety control air and both open to A-Auto. ABSCE. dampers fail closed on loss of control air. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
6.2.3-61 WBNP-112 | |||
ABGTS.Stuck open, fails to close, | Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 19 of 27) 6.2.3-62 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 34 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-30-130 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate the or spuriously Train B ABI or high rad isolation of cask Damper (0-FCO-30-129) and Train B cask loading area opens. in refueling area signal loading area 0-FCO-30-129 (0-FCO-30-130) dampers, in supply and to establish failure; HS failure to supply. provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air and both open to A-Auto. maintains the dampers fail closed on loss of ABSCE. control air. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table. | ||
Indicating light in | Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | ||
35 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-31-350 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate PASF or spuriously Train A ABI or high rad isolation of PASF Damper (0-FCO-31-350) and Train B outside air intake and to opens. in refueling area signal outside air intake. 0-FCO-31-365 (0-FCO-31-365) dampers are in establish boundary for failure; HS failure to provides series. Independence of Train A ABGTS. spring return from isolation and and Train B isolation signals is open to A-Auto. maintains the discussed in "Remarks" under ABSCE. Items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
Instrumentation Requirements WBNP-112 | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 20 of 27) | |||
Indicating light in | Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 36 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-31-365 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate PASF or spuriously Train B ABI or high rad isolation of PASF Damper (0-FCV-31-350) and Train B outside air intake and to opens. in refueling area signal outside air intake. 0-FCO-31-350 (0-FCV-31-365) dampers are in establish boundary for failure; HS failure to provides series. Independence of Train A ABGTS. spring return from isolation and and Train B isolation signals is open to A-Auto. maintains the discussed in "Remarks" under ABSCE. Items 1 and 2 of this table. | ||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
37 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1,2-FCO-31-342 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate PASF or spuriously Train A ABI or high rad isolation of PASF Damper 1,2- (1,2-FCO-31-342) and Train B Room No. 1 exhaust opens. in refueling area signal Room No. 1 FCO-31-343 (1,2-FCO-31-343) dampers are in and to establish failure; HS failure to exhaust. provides series. Independence of Train A boundary for ABGTS. spring return from isolation and and Train B isolation signals is open to A-Auto. maintains the discussed in "Remarks" under ABSCE. Items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation. | |||
38 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1,2-FCO-31-343 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate PASF or spuriously Train B ABI or high rad isolation of PASF Damper 1,2- (1,2-FCO-31-342) and Train B Room No. 1 exhaust opens. in refueling area signal Room No. 1 FCO-31-342 (1,2-FCO-31-343) dampers are in and to establish failure; HS failure to exhaust. provides series. Independence of Train A boundary for ABGTS. spring return from isolation and and Train B isolation signals is open to A-Auto. maintains the discussed in "Remarks" under ABSCE. Items 1 and 2 of this table. | |||
Damper failure to open is not listed since the damper has no safety WBNP-112 function to open for DBE 6.2.3-63 mitigation. | |||
ABGTS. | Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 21 of 27) 6.2.3-64 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 39 Modulating Regulates the amount Allows more Train A vital ac power "Hi Press. in Aux. See "Remarks" None. See ABI signal stops AB gen supply Damper of outside air to outside air failure; Train A aux. Bldg." alarm. column. "Remarks" fans automatically. The Aux. Bldg. | ||
0-FCO-30-149 maintain ABSCE at than required control air failure; column. is designed for minimum leakage Train A -0.25 in w.g. (stuck open or spurious high dP and, with at least one ABGTS spuriously signal; failure of E/I or exhaust fan running, failure of the excessive) I/P converter; modulating damper can cause positioner mechanical pressure in the Aux. Bldg. to failure. approach outside pressure, but the AB pressure cannot become positive with respect to the outside. | |||
The DPIS used for alarm in the control room is separate and independent from the DPIS used for modulating control of the damper. If the (non-safety) alarm functions, the operator can either close the associated Isolation Damper 0-FCO-30-280 or, if only one ABGTS exhaust fan is in operation, can start the redundant fan to maintain the -0.25 in w.g. | |||
pressure. | |||
Does not allow Train A vital ac power None. None (See Modulating Dampers the required failure; Train A aux. Train B Modulating note on items 0-FCO-30-148 and amount of control air failure; Damper 3 and 4.) 0-FCO-30-149 are provided with outside air spurious dP signal; 0-FCO-30-148 will train-separated, safety-grade (Stuck closed from 0-FCO-30-149; open to allow auxiliary control air. | |||
or spurious failure of E/I or I/P sufficient outside inadequate converter; positioner air to control the opening). mechanical failure. negative pressure. | |||
Instrumentation Requirements WBNP-112 | |||
ABGTS. | Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 22 of 27) | ||
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 40 Modulating Regulates the amount Allows more Train B vital ac power "Hi Press. in Aux. See "Remarks" None. See ABI signal stops AB gen supply Damper of outside air to outside air failure; Train B aux. Bldg." alarm. column. "Remarks" fans automatically. The Aux. Bldg. | |||
0-FCO-30-148 maintain ABSCE at than required control air failure; column. is designed for minimum leakage Train B -0.25 in w.g. (stuck open or spurious high dP and, with no air coming in and with spuriously signal; failure of E/I or at least one ABGTS exhaust fan excessive I/P converter; running, failure of the modulating opening). positioner mechanical damper can result in pressure in failure. the Aux. Bldg. approaching outside pressure, but the AB pressure cannot become positive with respect to the outside. The DPIS used for alarm in the control room is separate and independent from the DPIS used for modulating control of the damper. If the (non-safety) alarm functions, operator can either close the associated Isolation Damper 0-FCO-30-280 or, if only one ABGTS exhaust fan is in operation, can start the redundant fan to maintain -0.25 in w.g. | |||
Does not allow Train B vital ac power None. None (See Modulating Dampers the required failure; Train B aux. Train A Modulating note on items 0-FCO-30-148 and amount of control air failure; Damper 3 and 4.) 0-FCO-30-149 are provided with outside air spurious dP signal; 0-FCO-30-149 will train-separated, safety-grade (Stuck closed from 0-FCO-30-149; open to allow auxiliary control air. | |||
or spurious failure of E/I or I/P sufficient outside inadequate converter; positioner air to control the opening). mechanical failure. negative pressure. | |||
6.2.3-65 WBNP-112 | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 23 of 27) 6.2.3-66 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 41 ABGTS Vacuum Provides flow path for Fails to open, Mechanical failure; Indicating light in Aux. Bldg. at more None. See Dampers 0-FCO-30-279 and Relief Line outside air. stuck closed, Train A power failure; the MCR. negative pressure "Remarks" 0-FCO-30-280 are provided with Isolation Damper or spuriously Train A aux. control air (lower absolute column. train-separated, safety-grade 0-FCO-30-280 closes. failure; operator error pressure) than auxiliary control air. In addition, Train A (HS in wrong position). required to prevent there are two vacuum breaker leakage from dampers, 0-DMP-30-1128 and 0-outside. DMP-30-1129 in series which will admit outside air into the Bldg in case of increasing vacuum (more negative pressure). | |||
ITEM | Fails to close, Mechanical failure; Indicating light in None. Modulating None. The modulating damper cannot stuck open, or operator error (HS in the MCR. Damper shut off outside air completely. | ||
spuriously wrong position). 0-FCO-30-149 can However, the amount of air passed opens. independently will be insignificant to cause control amount of pressure control problem. | |||
outside air. | |||
42 ABGTS Vacuum Provides flow path for Fails to open, Mechanical failure; Indicating light in Aux. Bldg. at more None. See Dampers 0-FCO-30-279 and Relief Line outside air. stuck closed, Train B power failure; the MCR. negative pressure "Remarks" 0-FCO-30-280 are provided with Isolation Damper or spuriously Train B aux. control air (lower absolute column. train-separated, safety-grade 0-FCO-30-279 closes. failure; operator error pressure) than auxiliary control air. In addition, Train B (HS in wrong position). required to prevent there are two vacuum breaker leakage from dampers, 0-DMP-30-1128 and 0-outside. DMP-30-1129 in series which will admit outside air into the Bldg in case of increasing vacuum. | |||
Fails to close, Mechanical failure; Indicating light in None. Modulating None The modulating damper cannot stuck open, or operator error (HS in the MCR. Damper shut off outside air completely. | |||
spuriously wrong position). 0-FCO-30-148 can However, the amount of air passed Instrumentation Requirements opens. independently will be insignificant to cause control amount of pressure control problem. | |||
outside air. | |||
WBNP-112 | |||
ABGTS. | Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 24 of 27) | ||
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 43 Train A Provides Class 1E Loss of or Diesel generator Alarm and Loss of None. Train A isolation dampers are not Emergency diesel-backed power inadequate failure; bus fault indication in the redundancy in Redundant directly affected since damper Power supply to active voltage. (Train A); operator MCR. ABGTS exhaust Train B solenoids and control circuits are components of Train A error. flow paths. exhaust fan supplied either battery power or of ABGTS. can maintain battery-backed vital ac power. | |||
required Loss of power to the damper negative control circuits does not result in pressure. loss of redundancy since circuits are such that isolation dampers fail closed. | |||
44 Train B Provides Class 1E Loss of or Diesel generator Alarm and Loss of None. Train B isolation dampers are not Emergency diesel-backed power inadequate failure; bus fault indication in the redundancy in Redundant directly affected since damper Power supply to active voltage. (Train B); operator MCR. ABGTS exhaust Train A solenoids and control circuits are components of Train B error. flow paths. exhaust fan supplied either battery power or of ABGTS. can maintain battery-backed vital ac power. | |||
required Loss of power to the damper negative control circuits does not result in pressure. loss of redundancy since circuits are such that isolation dampers fail closed. | |||
45 Aux. Bldg. Provides flow path for Fails to open; Mechanical Failure Visual Aux. Bldg at more None. This damper will only be used in vacuum relief outside air. stuck closed. negative pressure the event that isolation dampers damper (lower absolute 0-DMP-30-279 and 0-DMP-30-280 0-DMP-30-1128 pressure) than fail close. Therefore, for this required to prevent damper to fail close, and one of the leakage to outside. isolation dampers to fail close at the same time would constitute a double failure. | |||
Fails to close, Mechanical Failure Visual None. Vacuum relief dampers stuck open. Vacuum relief 0-DMP-30-1128 and damper 0-DMP-30-1129 are installed in 0-DMP-30-1129 series. | |||
can close independently and WBNP-112 eliminate flow path from outside air. | |||
6.2.3-67 | |||
ABGTS. | Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 25 of 27) 6.2.3-68 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 46 Aux. Bldg. Provides flow path for Fails to open; Mechanical Failure Visual Aux. Bldg. at more None. This damper will only be used in vacuum relief outside air. stuck closed. negative pressure the event that isolation damper damper (lower absolute 0-DMP-30-279 and 0-DMP-30-280 0-DMP-30-1129 pressure) than fail close. Therefore, for this required to prevent damper to fail close, and one of the leakage to outside. isolation dampers to fail close at the same time would constitute a double failure. | ||
Fails to close; Mechanical Failure Visual None. Vacuum None (See Vacuum relief damper stuck open. relief damper Remarks) 0-DMP-30-1128 and 0-DMP-30-1128 0-DMP-30-1129 are installed in can close series. | |||
independently and eliminate flow path from outside air. | |||
Instrumentation Requirements WBNP-112 | |||
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 26 of 27) | |||
ITEM | Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 47 Fire Dampers Provide air flow path for Spurious Failure of fusible link. Low flow alarm. Loss of Train B None (See Fire dampers are safety-related; 0-ISV-31-3834 common duct between closure. Remarks). their failure constitutes a single and ABGTS fans. failure. Therefore, both ABGTS 0-ISV-31-3845 trains would be available. | ||
48 Deluge System Floods the carbon Spurious Failure of fusible link. ----- None (See None (See Opposite train ACU is independent (Spray heads adsorbers in event of opening of Remarks) Remarks). and remains available, or deluge and piping inside fire. spray heads, Loss of piping valve remains closed in the ACU A-A or B-B) or piping pressure boundary. absence of heat detection. | |||
failure 48b Deluge Valve Discharge water in Spurious - Mechanical failure Local and MCR None (See None (See ACU will not be flooded since the 1-FCV-26-163 event of fire in carbon actuation or alarms on water Remarks) Remarks) fusible links on the spray heads will adsorbers. - Electrical failure discharge be intact due to absence of heat. | |||
48c Deluge Valve Discharge water in Spurious - Mechanical failure Local and MCR None (See None (See ACU will not be flooded since the 2-FCV-26-171 event of fire in carbon actuation or alarms on water Remarks) Remarks) fusible links on the spray heads will adsorbers. - Electrical failure discharge be intact due to absence of heat. | |||
49 Ductwork in the Provides containment Leakage. Cracks. ---- Minimal localized None (See Only small cracks are postulated ABSCE for air flow path. reduction of Remarks) due to seismic qualification. | |||
negative pressure. Minimal localized reduction of negative pressure will not affect the ABSCE. | |||
Loss of fluid (air) is not a concern since the system is submerged in the same fluid. | |||
6.2.3-69 WBNP-112 | |||
ABGTS. | Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 27 of 27) 6.2.3-70 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 50 ABGTS Air Controls humidity of Fails to turn on Train A power failure; Hi Rad alarm in the Loss of None (See 1. Failure to cutout is not Cleanup Unit A exhaust air. or fails to temperature sensing MCR for air to redundancy in Remarks) considered in this table since Heater operate. error. Shield Bldg. vent. ABGTS. Failure of this is the safe position for heater will allow controlling air humidity. | ||
humid air into carbon filter 2. The air temperature for the reducing its switch, 0-TS-30-143, for this efficiency (see heater is sensed by a "Remark #3"). non-safety related sensor, 0-TE-30-143. DCN M-21750 has been initiated to resolve this problem. Section 8.2 address this further. | |||
: 3. Heater operation is tested every 31 days per procedure. | |||
51 ABGTS Air Controls humidity of Fails to turn on Train B power failure; Hi Rad alarm in the Loss of None (See 1. Failure to cutout is not Cleanup Unit B exhaust air. or fails to temperature sensing MCR for air to redundancy in Remarks) considered in this table since Heater operate. error. Shield Bldg. vent. ABGTS. Failure of this is the safe position for heater will allow controlling air humidity. | |||
humid air into carbon filter 2. The air temperature for the reducing its switch, 0-TS-30-143, for this efficiency (see heater is sensed by a "Remark #3"). non-safety related sensor, 0-TE-30-143. DCN M-2175 has been initiated to resolve this problem. Section 8.2 address this further. | |||
: 3. Heater operation is tested every Instrumentation Requirements 31 days per procedure. | |||
WBNP-112 | |||
ABGTS. | Instrumentation Requirements WATTS BAR Table 6.2.3-3 Failure Modes and Effects Analysis for the ABGTS NOTES FOR ABGTS FAN FAILURE MODES AND THEIR IMPACT ON THE EGTS POST-ACCIDENT TIME INTERVAL EGTS ABGTS REMARKS 0 - 30 minutes 2 fans (auto start) 2 fans (auto start) 2 EGTS fans together produced -2.3 w.g. dP in the annulus more than the dP of | ||
-0.69 w.g. effected by the ABGTS fans in ABSCE. | |||
1 fan operating 2 fans (auto start) 2 ABGTS fans together pulled a vacuum of -0.69 w.g. @ Elevation 763.0 of the ABSCE, whereas, 1 EGTS fan drew down the annulus to -1.15 w.g., thus attesting 1 fan failed that the annulus dPs are more negative than ABSCE. | |||
2 fans (auto start) 2 fans (auto start) 2 ABGTS fans together drew down the ABSCE to -1.09 w.g. @ Elevation 763.0 of the ABSCE, whereas, the 2 EGTS fan together produced -2.3 w.g. in the annulus. | |||
Therefore, the annulus dP remains more negative. | |||
1 fan operating 2 fans (auto start) The failure of two safety-related components (i.e., fan and a damper affecting the same parameter, namely the annulus dP, is not postulated. Therefore, this failure mode is invalid. | |||
> 30 minutes 1 fan (operating) 1 fan (operating) 1 EGTS fan produces more negative dP in the annulus than 1 ABGTS fan in the ABSCE 1 fan (shutdown by operator) 1 fan (shutdown by operator) 1 fan (operating) 1 fan (operating) 2 ABGTS fans together produced a dP of -0.69 w.g. @ Elevation 763.0 of AB; whereas, 1 EGTS fan drew down the annulus to -1.15 w.g. @ Elevation 783.0. | |||
Therefore, the annulus is more negative than ABSCE. | |||
1 fan (operating) 2 fans (operator is yet to shutdown 2 ABGTS fans together drew down the ABSCE to -1.09 w.g. @ Elevation 763.0, one of the fans) whereas 1 EGTS fan was able to maintain -1.15 w.g. @ Elevation 783.0 of the annulus. However, in a later test, the same EGTS fan maintained -1.05 w.g. | |||
1 fan (shutdown by operator) 1 vacuum relief damper failed However, the dP in the ABSCE remained less negative than that of the annulus. | |||
6.2.3-71 WBNP-112 | |||
Table 6.2.3-3 Failure Modes and Effects Analysis for the ABGTS 6.2.3-72 WATTS BAR NOTES FOR ABGTS FAN FAILURE MODES AND THEIR IMPACT ON THE EGTS POST-ACCIDENT TIME INTERVAL EGTS ABGTS REMARKS 0 - 30 minutes 2 fans (auto start) 2 fans (auto start) 2 EGTS fans together produced -2.3 w.g. dP in the annulus more than the dP of - | |||
0.69 w.g. effected by the ABGTS fans in ABSCE. | |||
1 fan operating 2 fans (auto start) 2 ABGTS fans together pulled a vacuum of -0.69 w.g. @ Elevation 763.0 of the ABSCE, whereas, 1 EGTS fan drew down the annulus to -1.15 w.g., thus attesting 1 fan failed that the annulus dPs are more negative than ABSCE. | |||
2 fans (auto start) 2 fans (auto start) 2 ABGTS fans together drew down the ABSCE to -1.09 w.g. @ Elevation 763.0 of the ABSCE, whereas, the 2 EGTS fan together produced -2.3 w.g. in the annulus. | |||
Therefore, the annulus dP remains more negative. | |||
1 fan operating 2 fans (auto start) The failure of two safety-related components (i.e., fan and a damper affecting the same parameter, namely the annulus dP, is not postulated). Therefore, this failure mode is invalid. | |||
Instrumentation Requirements WBNP-112 | |||
WATTS BAR WBNP-112 Figure 6.2.3-1 Typical Mechanical Penetration Seals Secondary Containment Functional Design 6.2.3-73 | |||
WATTS BAR WBNP-112 Figure 6.2.3-2 Typical Purge Penetration Arrangement Secondary Containment Functional Design 6.2.3-74 | |||
WATTS BAR WBNP-112 Figure 6.2.3-3 Typical Electrical Penetrations Secondary Containment Functional Design 6.2.3-75 | |||
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-4 Auxiliary Building Isolation Barrier Secondary Containment Functional Design 6.2.3-76 | |||
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-5 Auxiliary Building Isolation Barrier Secondary Containment Functional Design 6.2.3-77 | |||
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-6 Auxiliary Building Isolation Barrier Secondary Containment Functional Design 6.2.3-78 | |||
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-7 Auxiliary Building Isolation Barrier Secondary Containment Functional Design 6.2.3-79 | |||
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-8 Auxiliary Building Isolation Barrier Secondary Containment Functional Design 6.2.3-80 | |||
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-9 Auxiliary Building Isolation Barrier Secondary Containment Functional Design 6.2.3-81 | |||
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-10 Auxiliary Building Isolation Barrier Secondary Containment Functional Design 6.2.3-82 | |||
WATTS BAR Secondary Containment Functional Design Figure 6.2.3-11 Reactor Building - Units 1 & 2 Flow Diagram - Heating and Ventilation Air Flow WBNP-112 6.2.3-83 | |||
WATTS BAR Secondary Containment Functional Design Figure 6.2.3-12 Powerhouse Units 1 & 2 Electrical Logic Diagram - Emergency Gas Treatment System WBNP-112 6.2.3-84 | |||
WATTS BAR Secondary Containment Functional Design Figure 6.2.3-13 Powerhouse Units 1 & 2 Electrical Logic Diagram - Emergency Gas Treatment WBNP-112 6.2.3-85 | |||
WATTS BAR Secondary Containment Functional Design Figure 6.2.3-14 Powerhouse Unit 1 Electrical Logic Diagram -Emergency Gas Treatment WBNP-112 6.2.3-86 | |||
WATTS BAR Secondary Containment Functional Design Figure 6.2.3-15 Powerhouse Units 1 & 2 Electrical Control Diagram - Emergency Gas Treatment System WBNP-112 6.2.3-87 | |||
WATTS BAR Secondary Containment Functional Design Figure 6.2.3-15-SH-A Powerhouse Unit 2 Electrical Control Diagram - Emergency Gas Treatment WBNP-112 6.2.3-88 | |||
WATTS BAR Secondary Containment Functional Design Figure 6.2.3-16 Powerhouse Units 1 & 2 Auxiliary Building -Flow Diagram -Heating & Ventilating Air Flow WBNP-112 6.2.3-89 | |||
WATTS BAR Secondary Containment Functional Design Figure 6.2.3-17A Post-Accident Annulus Pressure and Vent Flow Rate WBNP-112 6.2.3-90 | |||
WATTS BAR WBNP-112 Figure 6.2.3-17 Post-Accident Annulus Pressure and Reactor Unit Vent Flow Rate Transients Secondary Containment Functional Design 6.2.3-91 | |||
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-18 Reactor Building Units 1 & 2 Mechanical Heating and Ventilating Secondary Containment Functional Design 6.2.3-92 | |||
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-19 Reactor Building Units 1 & 2 Mechanical Heating, Ventilation, And Air Conditioning Secondary Containment Functional Design 6.2.3-93 | |||
WATTS BAR WBNP-112 THIS PAGE INTENTIONALLY BLANK Secondary Containment Functional Design 6.2.3-94 | |||
closed. | WATTS BAR WBNP-112 6.2.4 Containment Isolation Systems The containment isolation systems provide the means of isolating fluid systems that pass through containment penetrations so as to confine to the containment any radioactivity that may be released in the containment following a design basis event. | ||
The containment isolation systems are required to function following any design basis event that initiates a Phase A or Phase B containment isolation signal or releases radioactive materials into containment to isolate non-safety-related fluid systems penetrating the containment. The Watts Bar Nuclear Plant does not have a particular system for containment isolation, but isolation design is achieved by applying common criteria to penetrations in many different fluid systems and by using ESF signals to actuate appropriate valves. | |||
6.2.4.1 Design Bases The main function of the containment isolation system is to provide containment integrity when needed. Containment integrity is defined to exist when: | |||
(1) The non-automatic containment isolation valves and blind flanges are closed as required. | |||
(2) The containment equipment hatch is properly closed. | |||
(3) At least one door in each containment personnel air lock is properly closed. | |||
(4) All automatic containment isolation valves are operable or are deactivated in the closed position or at least one valve in each line having an inoperable valve is closed. | |||
(5) All requirements of the Technical Specification with regard to containment leakage and test frequency are satisfied. | |||
Containment integrity is required if there is fuel in the reactor which has been used for power operation, except when the reactor is in the cold shutdown condition with the reactor vessel head installed, or when the reactor is in the refueling shutdown condition with the reactor vessel head removed. Containment isolation is not essential for design basis events, such as HELBs, outside containment which do not release radioactive materials into containment. The failure of containment isolation valves for such an event would not result in the release of radioactive fluids from inside containment. | |||
In general, the containment isolation system is designed to the requirements of General Design Criteria 54, 55, 56, and 57 of 10 CFR 50, Appendix A. The following are alternate containment isolation provisions for certain classes of lines: | |||
(1) Fluid instrument lines penetrating the containment are designed to meet the referenced General Design Criteria except for the pressure sensor and reactor vessel level instrumentation system lines. Instrument lines which penetrate containment are listed in Table 6.2.4-4. | |||
Containment Isolation Systems 6.2.4-1 | |||
WATTS BAR WBNP-112 (2) Remote-manual valves are used for isolation provisions on certain lines associated with engineered safety features (such as the ECCS) instead of automatic isolation valves. | |||
(3) A closed system outside the containment is acceptable as one of the two isolation barriers if designed to the following criteria: | |||
(a) Does not communicate with the outside environment (b) Meets Safety Class 2 design requirements (c) Withstands the internal temperatures and pressures which occur as a result of the containment design basis events (d) Withstands loss-of-coolant accident transients and environment (e) Meets Seismic Category I design requirements (f) Protected against missiles, pipe whip, and jet impingement. | |||
(4) The isolation function of an engineered safety feature or system required to test an engineered safety feature requires one barrier to remain functional after the occurrence of a single active failure. Normally, this is accomplished by providing two isolation valves in series. If it can be shown that a single active failure can be accommodated with only one valve in the line and that fluid system reliability is enhanced by having one valve rather than two valves in series, then one valve and a closed system both located outside of the containment are acceptable. The single valve and piping between the containment and the valve are enclosed in a protective leaktight housing to prevent leakage to the atmosphere in the event of external leakage. | |||
(5) Relief valves may be used as isolation valves, provided the relief valve setpoint is greater than 1.5 times the containment design internal pressure. | |||
The criteria for the number and location of containment isolation valves in each fluid system depend on the valves functions and whether they are open or closed to the containment atmosphere or reactor coolant system. Four isolation classes of fluid system penetrations are defined as follows: | |||
(1) Isolation Class I - Fluid lines which are open to the atmosphere outside the containment and are connected to the reactor coolant system or are open to the containment atmosphere. Each isolation Class I system has a minimum of two isolation valves in series. Where system design permits, one valve is located inside and one valve is located outside containment. | |||
(2) Isolation Class II - Fluid lines which are connected to a closed system outside the containment and are connected to the reactor coolant system or are open to the containment atmosphere. Also included in isolation Class II are fluid lines which are open to the atmosphere outside the containment and are 6.2.4-2 Containment Isolation Systems | |||
the | WATTS BAR WBNP-112 separated from the reactor coolant system and the containment atmosphere by a closed system inside the containment. Each isolation Class II system has, as a minimum, one isolation valve. | ||
(3) Isolation Class III - Fluid lines which are connected to a closed system both inside and outside the containment. Isolation Class III systems have, as a minimum, one isolation valve. | |||
(4) Isolation Class IV - Fluid lines which must remain in service subsequent to a design basis event, such as lines serving ESF systems. Isolation valves on these lines are not automatically closed by the containment isolation signal. | |||
Each isolation Class IV system has, as a minimum, one isolation valve (remote-manual operation). | |||
The following design requirements for containment isolation barriers apply: | |||
(1) The design pressure of all piping and connected equipment comprising the isolation boundary is equal to or greater than the design pressure of the containment. | |||
(2) All valves and equipment which are considered to be isolation barriers and designed in accordance with Seismic Category I criteria shall be protected against missiles and jet impingement, both inside and outside the containment. | |||
(3) All valves and equipment which are considered to be isolation barriers are designed, as a minimum, to ASME Section III Class 2 requirements except as noted in Item 1 of Section 6.2.4.2.1. | |||
(4) A system is closed inside the containment if it meets all of the following: | |||
(a) It does not communicate with either the reactor coolant system or the reactor containment atmosphere. | |||
(b) It will withstand external pressure and temperature equal to containment structural integrity test pressure and design temperature. | |||
(c) It will withstand accident temperature, pressure, and fluid velocity transients, and the resulting environment, including internal thermal expansion. | |||
(d) It is protected against missiles, pipe whip, and jet impingement. | |||
(5) A check valve inside the containment on the incoming line is considered an automatic isolation valve. | |||
(6) A pressure relief valve that relieves toward the inside of the containment is considered an automatic isolation valve. | |||
(7) A locked closed valve is considered an automatic isolation valve. | |||
Containment Isolation Systems 6.2.4-3 | |||
WATTS BAR WBNP-112 (8) To qualify as an automatic isolation valve, an air-operated valve must fail closed on loss of air, power, etc. | |||
(9) Valves used for containment isolation shall be designed capable of tight shutoff in order to limit gas leakage to a specific maximum amount at containment design pressure. | |||
The design bases for the containment isolation system include provision for the following: | |||
(1) A double barrier at the containment penetration in those fluid systems that are not required to function following a design basis event. | |||
(2) Automatic, fast, efficient closure of those valves required to close for containment integrity following a design bases event to minimize release of any radioactive material. | |||
(3) A means of leak testing barriers in fluid systems that serve as containment isolation. | |||
(4) The capability to periodically test the operability of containment isolation valves. | |||
6.2.4.2 System Design The containment isolation system meets the design bases presented in Section 6.2.4.1 with the exception of those cases which are discussed in detail in Section 6.2.4.3. | |||
Containment isolation can be initiated by either Phase A or Phase B signals. | |||
A Phase A signal is generated by either of the following: | |||
(1) Manual - either of two momentary controls (2) A safety injection signal, generated by one or more of the following: | |||
(a) Low steamline pressure in any steamline (b) Low pressurizer pressure (c) High containment pressure (d) Manual - either of two momentary controls. | |||
6.2.4-4 Containment Isolation Systems | |||
WATTS BAR WBNP-112 A Phase B signal is generated by either of the following: | |||
(1) Manual - two sets (two switches per set) - actuation of both switches is necessary in either set for spray initiation (2) Automatic High-high containment pressure. | |||
Containment isolation Phase A always exists if containment isolation Phase B exists, when the Phase B signal is initiated by automatic instrumentation. Phase A containment isolation does not occur when the Phase B signal is initiated manually. | |||
The instrumentation circuits that generate both Phase A and Phase B signals are described in Chapter 7. | |||
With the exception of the cases identified below, the containment isolation system provides for automatic, fast, and efficient closure of those valves required to close for containment integrity following a design basis event to minimize the release of any radioactive material. Closure times for isolation valves are included in Table 6.2.4-1. | |||
With a single failure of containment isolation valves 1-FCV-32-110, 1-FCV-67-107, 1FCV-70-92 or 1-FCV-70-140, concurrent with an HELB inside containment such as a LOCA, Main Steam Line Break, or Feedwater Line Break, etc., manual actions are required to prevent the possibility of process fluid (air or water) from entering containment (See Tables 9.2-2, 9.2-9, and 9.3-7). Manual actions are required in these cases since a check valve serves as an inboard containment isolation valve, and pressure boundary integrity of the lines in containment past the check valves cannot be assured. | |||
6.2.4.2.1 Design Requirements Containment isolation barrier design includes the following requirements: | |||
(1) As a minimum, containment barriers are designed to ASME Section III Class 2 requirements. This design meets the requirements of Regulatory Guide 1.26 for the containment isolation systems, except that the four auxiliary feedwater lines incorporate safety-grade Quality Group C (ASME Section III, Class 3) valves outside containment for isolation. This has been documented in NUREG 0847 as acceptable to the NRC. Valves and equipment which are considered to be isolation barriers are designed to Seismic Category I requirements which is the intent of Regulatory Guide 1.29. | |||
(2) Isolation barriers either inside or outside of the containment are protected against missiles, pipe whip, and jet impingement during a LOCA. | |||
(3) Power operated isolation valves are tested for operability by the manufacturer and preoperationally after installation. Those automatic isolation valves with air or motor operators that do not restrict normal plant operation are periodically tested to ensure operability. | |||
Additional design information is included in Table 6.2.4-1. | |||
Containment Isolation Systems 6.2.4-5 | |||
and | WATTS BAR WBNP-112 6.2.4.2.2 Containment Isolation Operation A containment isolation signal initiates closing of automatic isolation valves in those lines which must be isolated immediately following a design basis event. The containment isolation valves will close within the time specified in Table 6.2.4-1. | ||
However, on loss of ac power, the diesel will have to be started prior to closure. It is estimated that the time required to start the diesel is 10 seconds. The logic diagram for this system is shown in Figure 6.2.4-21. | |||
Check valves are used under conditions where differential pressure will close the valves to maintain containment integrity. Lines which, for safety reasons, must remain in service subsequent to a design basis event are provided with at least one isolation valve. | |||
Each automatic isolation valve required to operate subsequent to an accident is additionally provided with a manual control switch for operation. The position of these automatic isolation valves is indicated by status lights in the main control room. | |||
Primary and secondary modes of valve actuation are shown in Table 6.2.4-1. | |||
Redundant isolation barriers are used to prevent any single failure from causing an open path from the containment. If two power operated valves are used in series in a line for isolation purposes, one valve is supplied with one train of control and power and the other valve is supplied by the other train. Redundancy in power, signals, and barriers is provided to assume isolation. | |||
Provisions for detecting leakage from remote manually controlled systems (such as the ECCS) include the use of pressure and flow meters, and inspection of the systems during normal plant operation. Details for leak detection are given in the appropriate system descriptions. Piping systems penetrating the containment have been provided with test vents and test connections or have other provisions to allow periodic leak testing (see Section 6.2.6). Test connections, vents and drains located within the containment boundary (between containment isolation valves) of penetrations subject to 10CFR50, Appendix J, Type C testing also have the capability of being leak tested or are one inch in size or less, administratively secured closed and consist of a double barrier (e.g. two valves in series, one valve with nipple and cap, one valve and a blind flange). | |||
The manufacturers of isolation system components perform tests to demonstrate the ability of mechanical and electrical components located inside the containment to perform as required in the containment environment following the design basis accident. Accident conditions which are considered in the design of isolation components are pressure, humidity, radiation, and temperature. Section 3.11 gives information concerning the environmental conditions used in the design of the containment isolation system including more detail on qualification testing of ESF components. | |||
The description and design requirements for the instrumentation and control portions of the containment isolation system are discussed in Chapter 7. | |||
6.2.4-6 Containment Isolation Systems | |||
WATTS BAR WBNP-112 6.2.4.2.3 Penetration Design The penetrations are classified into 24 different types. These are shown in Figures 6.2.4-1 through 6.2.4-17E. | |||
The locations of these penetrations through the steel containment and the Shield Building are shown in Figures 6.2.4-18 and 6.2.4-19, respectively. The penetrations are tabulated in Table 6.2.4-1. The different types of penetrations are discussed below and the various possible leakage paths, as tabulated in Table 6.2.4-1 and shown in Figure 6.2.4-20, are also described below. | |||
Penetration Types I and II - Main Steam and Feedwater The main steam and feedwater line penetrations, shown in Figures 6.2.4-1 and 6.2.4-2, are the "hot" type in which the penetrations must accommodate thermal movement. Each "hot" process line where it passes through the containment penetration is enclosed in a guard pipe that is attached to the process line through a multiple fluid fitting. The guard pipe protects the bellows should the process line fail within the annulus between the containment vessel and the Shield Building, thereby precluding the discharge of fluids into the annulus. The inner end of the guard pipe is fitted with an impingement ring which protects the bellows from jets originating from pipe breaks inside containment. In addition, the guard pipe for this type of penetration extends through and is supported by the crane wall. This avoids transmitting loads to the containment vessel. Also, in the event of a pipe rupture it discharges fluid into the reactor compartment rather than smaller rooms outside the crane wall, thus preventing, overpressurization of these smaller rooms. | |||
For each of these penetrations the penetration sleeve is welded to the containment vessel. The process line which passes through the penetration is allowed to move both axially and laterally. A two-ply bellows expansion joint is provided to accommodate any movement between the containment vessel and the Shield Building, under any conditions. The bellows is designed to withstand containment design pressure. When an embedded anchor is not utilized, a low-pressure flexible closure will seal the process line to the sleeve in the Shield Building, which will not impose significant stress on the penetration. | |||
The flexible closure described above is located outdoors and serves to contain leakage from the flued head so that the leakage is routed back to the annulus, and to seal the annulus from the outdoors. | |||
Guides and anchors limit movement of pipes such that design limits on the containment penetration and bellows are not exceeded during conditions of plant operation, test, or postulated accidents. | |||
Penetration Type III - Residual Heat Removal Pump Supply and Return The RHR pump supply and return penetrations, shown in Figure 6.2.4-3, are also the "hot" type. For these penetrations, the guard pipe does not penetrate the crane wall. | |||
This type of penetration is anchored at the Shield Building wall in addition to being Containment Isolation Systems 6.2.4-7 | |||
WATTS BAR WBNP-112 supported from the internal concrete structure to minimize loads transmitted to the steel containment vessel. | |||
- | The Shield Building sleeves have embedded anchors and the flued heads are in the Auxiliary Building. There is no need for low-pressure flexible closures as used in penetrations types I and II, since any leakage from the flued head will be processed by the auxiliary building gas treatment system. | ||
Penetration Types IV and V Types IV and V penetrations are also thermally "hot" with insulation and bellows, as shown in Figure 6.2.4-4. Any leakage through the flued heads or through the bellow will be into the annulus and thereby processed by the emergency gas treatment system. The two types differ by only the weld ends. | |||
Penetration Types VI, VII, and VIII Penetrations types VI through X and XIII through XVIII are "cold" penetrations. | |||
For "cold" piping penetrations, a low-pressure flexible closure will seal the cold pipe to the sleeve penetrating the Shield Building. The piping configuration and supports on either side of the penetration will be designed to preclude overstressing the containment vessel at the penetration under any conditions, including postulated accidents. | |||
Relatively small thermal movement or stress is expected for the "cold" penetrations. | |||
The clearance space provided for the pipe going through the Shield Building wall is computed by the summation of the relative movements of the pipe and the Shield Building . Ample clearance space is provided so that the pipe will not be in contact with the Shield Building sleeve under any condition. | |||
Penetration types VI and VII have provisions for dissimilar metal welding. The two types differ in their weld ends only. Penetration types VI and VII are illustrated in Figure 6.2.4-5. The flued heads of both types are located in the annulus. | |||
Penetration type VIII is similar to that of penetrations types VI and VII, except that there is no dissimilar metal weld. Penetration type VIII is illustrated in Figure 6.2.4-6. | |||
Penetration Type IX Containment Spray and RHR Spray Headers There is no difference between penetration types VII and IX except that penetration type IX is located at the dome. Penetration type IX is illustrated in Figure 6.2.4-7. The flued heads are located in the annulus. | |||
Penetration Type X - Multiple Line Sleeves Type X penetrations are primarily for instrumentation lines such as sampling and monitor lines. Typical multiple line sleeves are shown in Figure 6.2.4-8. | |||
6.2.4-8 Containment Isolation Systems | |||
WATTS BAR WBNP-112 Penetration Types XI and XII - Emergency Sump During long-term post-accident conditions, containment sump water is recirculated through the RHR system and the containment spray system. The water collects on the floor of the containment and flows to the emergency sump. The water flows out of the containment through two type XII penetrations shown in Figure 6.2.4-9. Each line contains an isolation valve enclosed in a valve compartment. The valve compartments are designed for the same conditions as the containment except for leaktightness. The penetration between each valve compartment and the Auxiliary Building is a type XI penetration illustrated in Figure 6.2.4-10. | |||
- | The type XII penetration has a flued head located in the containment sump. The outer sleeve (guard pipe) of the flued head is welded directly to the containment liner which is completely embedded in the concrete. | ||
The type XI penetration has the flued head located in the Auxiliary Building. The penetration is insulated because of the hot sump water which would pass through it in the event of a design bases event. | |||
Penetration Type XIII - Ventilation Heating and ventilation ducts utilize penetration type XIII, as shown in Figure 6.2.4-11. | |||
Process lines are welded directly to these penetrations. Additional information on ventilation duct penetrations is given in Section 6.2.4.3.1 on possible leakage paths. | |||
Penetration Type XIV - Equipment Hatch An equipment hatch fabricated from welded steel and furnished with a double-gasketed flange and bolted dished door is provided. A test connection to the space between the gaskets is provided to pressurize the space for leak rate testing, as shown in Figure 6.2.4-12. | |||
Penetration Type XV - Personnel Access Two personnel air locks are provided. Each personnel air lock, as shown in Figure 6.2.4-13, is a double door welded steel assembly. Quick-acting type equalizing valves are provided to equalize pressure in the air lock when personnel enter or leave the containment vessel. The doors are sealed with double gaskets. A test connection to the space between the gaskets is provided to pressurize the space for leak rate testing. | |||
The emergency air supply connection to the space between the double doors serves as a test connection to pressurize this space for leak rate testing. A special hold-down device is provided to secure the inner door in a sealed position during leak rate testing of the space between the doors. | |||
The two doors in each personnel air lock are interlocked to prevent both being opened simultaneously and to ensure that one door and its equalizing valve are completely closed before the opposite door can be opened. Remote indicating lights and annunciators located in the main control room indicate the door is in operational status. | |||
Provision is made to permit bypassing the door interlocking system with a special tool to allow doors to be left, open during plant cold shutdown. Both doors may also be left Containment Isolation Systems 6.2.4-9 | |||
WATTS BAR WBNP-112 open during fuel handling activities under special administrative controls as discussed in Section 6.2.3.2.1. Each lock door hinge is designed to be capable of adjustment to assure proper seating. A lighting and communication system is provided in the lock interior. | |||
Penetration Type XVI - Fuel Transfer Tube A 20-inch OD fuel transfer tube penetration is provided for fuel movement between the refueling canal in the containment and the spent fuel pool. The penetration consists of 20-in stainless steel pipe installed inside a 24-inch carbon steel pipe, as shown on Figure 6.2.4-14. The inner pipe acts as the transfer tube and is fitted with a double gasketed blind flange in the refueling canal and a standard gate valve in the spent fuel pool. The inner pipe is welded to the containment penetration sleeve. Bellows expansion joints are provided on the pipes to compensate for any differential movement between the two pipes or other structures. | |||
Penetration Type XVII - Incore Instrumentation Thimble Assembly (IITA) | |||
Renewal Incore instrumentation thimble assembly (IITA) renewal requires penetrations in both the steel containment and the Shield Building at the same elevation and azimuth. | |||
These are separate penetrations and are not connected in the annulus. The containment penetration, illustrated in Figure 6.2.4-15, has a blind flange with double O-rings and a leak rate test connector installed inside the annulus. The shield building penetration utilizes a raised face blind flange with a single gasket installed outside the shield building. | |||
Penetration Type - XVIII - Ice Blowing The ice blowing line penetration has a blind flange with double O-rings installed on the outside of the containment as shown in Figure 6.2.4-16. Sealing between the outside and the annulus penetration through the shield wall is provided by a blind flange fitted with a gasket installed on the inside and outside of the Shield Building penetration. | |||
Penetration Type XIX - Electrical The electrical penetration assemblies provide a means for the continuity of power, control, and signal circuits through the primary containment structure. | |||
Each assembly consists of redundant pressure barriers through which the electrical conductors are passed, as shown in Figure 6.2.4-17. | |||
Each penetration assembly is sized such that it may be inserted into and be compatible with the penetration nozzles which are furnished as a part of the containment structure. | |||
Unless otherwise specified, the assembly is designed to be inserted from the outboard-end of the primary containment nozzle. | |||
The criteria and requirements for the design, construction, and installation of the modular type electrical penetrations conform to IEEE Standard 317-1976, "IEEE 6.2.4-10 Containment Isolation Systems | |||
WATTS BAR WBNP-112 Standard for Electrical Penetration Assemblies in Containment Structures for Nuclear Fueled Power Generating Stations." | |||
The criteria and requirements for the design construction and installation of fiber optic feed-throughs in modular type electrical penetrations conform to IEEE Standard 317-1983. IEEE Standard for Electric Penetration Assemblies in Containment Structures for Nuclear Power Generating Station. | |||
Penetration Type XX The feedwater bypass line penetrations, shown in Figure 6.2.4-17A are the 'hot' type in which the penetrations must accommodate thermal movement. Each 'hot' process line where it passes through the containment penetration is enclosed in a guard pipe that is attached to the process line through a multiple fluid fitting. The guard pipe protects the bellows should the process line fail within the annulus between the containment vessel, thereby precluding the discharge of fluids into the annulus. The inner end of the guard pipe is fitted with an impingement ring which protects the bellows from jets originating from pipe breaks inside containment. In addition, the guard-pipe for this type of penetration extends through and is supported by the crane wall. This avoids transmitting loads to the containment vessel. Also, in the event of a pipe rupture it discharges fluid into the reactor compartment rather than smaller rooms outside the crane wall, thus preventing overpressurization of these smaller rooms. | |||
For each of these penetrations, the penetration sleeve is welded to the containment vessel. The process line which passes through the penetration is allowed to move both axially and laterally. A two-ply bellows expansion joint is provided to accommodate movement between the containment vessel and the Shield Building. The bellows is designed to withstand containment design pressure. When an embedded anchor is not utilized, a low-pressure flexible closure will seal the process line to the sleeve in the Shield Building, which will not impose significant stress on the penetration. | |||
The flexible closure described above is located outdoors and serves to contain any leakage from the flued head so that the leakage is routed back to the annulus, and to seal the annulus from the outdoors. | |||
Guides and anchors limit movement of pipes such that design limits on the containment penetration and bellows are not exceeded during plant operation, testing, or postulated accidents. | |||
Penetration Type XXI The ERCW lines and several component cooling water lines employ penetration type XXI, as shown in Figure 6.2.4-17B. Process lines are welded directly to these penetrations. | |||
Penetration Type XXII The type XXII penetration is used for the multiple line nitrogen penetration. This penetration is shown in Figure 6.2.4-17C. | |||
Containment Isolation Systems 6.2.4-11 | |||
WATTS BAR WBNP-112 Penetration Type XXIII This type of penetration is used for the chilled water lines and each penetration contains a single chilled water line. The penetration is illustrated in Figure 6.2.4-17D. | |||
Penetration Type XXIV Type XXIV penetrations are used for maintenance ports. These penetrations employ bellows as shown in Figure 6.2.4-17E. Any leakage through the flued heads or through the bellows will be into the annulus and thereby processed by the emergency gas treatment system. | |||
The following codes, standards, and guides were applied in the design of the containment isolation system. | |||
(1) 10 CFR Part 50 (2) ASME Boiler and Pressure Vessel Code Section III (3) Regulatory Guide 1.26 (4) Regulatory Guide 1.29 (5) ANSI N18.2-August 1970 draft (6) IEEE Standard 317-1976 6.2.4.3 Design Evaluation The containment isolation systems are designed to present a double barrier to any flow path from the inside to the outside of the containment using the double-barrier approach to meet the single-failure criterion. | |||
When permitted by fluid system design, diverse modes of actuation are used for automatic isolation valves. In addition to diverse modes of operation, channel separation is also maintained. This also ensures that the single-failure criterion is met. | |||
Adequate protection is provided for piping, valves, and vessels against dynamic effects and missiles which might result from plant equipment failures, including a LOCA. | |||
( | Isolation valves inside the containment are located between the crane wall and the inside containment wall. The crane wall serves as the main missile barrier. Other missile barriers are discussed in Section 3.5. | ||
The requirements and intent of NRC General Design Criteria 54, 55, 56, and 57 have been met with five exceptions. | |||
(a) Primary containment monitoring instrument systems shall be designed to maintain the integrity of the containment isolation boundary in the event of a DBE. The instrument systems consist of pressure sensors (e.g., transmitters) located outside containment and associated sense 6.2.4-12 Containment Isolation Systems | |||
WATTS BAR WBNP-112 lines that connect to the containment penetration nozzles. The sensors should be located as close as practical to the associated penetration nozzle. Any drain or test line used shall meet the double isolation barrier by use of two normally closed manual valves in series. | |||
The instrument system shall be designed to Seismic Category I requirements and evaluated for effects of possible missiles, pipe whip, and jet impingement. | |||
(b.1) The reactor vessel level indication system (RVLIS) is required post accident for continual indication of the water level in the reactor vessel. | |||
The capillary sensing lines which transmit pressure from the reactor vessel to instruments in the Auxiliary Building are armored and designed to withstand DBE conditions. Any containment isolation valves installed in the RVLIS capillary lines will jeopardize the performance of the system. For this reason, isolation of these capillary lines is accomplished by a sealed sensor located inside containment and an isolator located outside containment. These devices utilize a type of bellows which transmits pressure while preventing mixing of the fluids on either side of the isolation devices. The capillary line is armored stainless steel tubing and is filled with demineralized water and sealed. A postulated shear of this capillary line on either side of the containment would not allow a leak to develop through the containment boundary. | |||
(b.2) The RCS wide range pressure transmitter (PT-68-70) is required post accident for continual indication of the pressure in the reactor vessel. | |||
The capillary sensing lines which transmit pressure from the reactor vessel to instruments in the Auxiliary Building are armored and designed to withstand DBE conditions. Any containment isolation valves installed in the RCS wide range pressure transmitter capillary lines will jeopardize the performance of the system. For this reason, isolation of these capillary lines is accomplished by a sealed sensor located inside containment and an isolator located outside containment. | |||
These devices utilize a type of bellows which transmits pressure while preventing mixing of the fluids on either side of the steel tubing and is filled and sealed. A postulated shear of this capillary line on either side of the containment would not allow a leak to develop through the containment boundary. | |||
(c) Containment isolation for each RHR sump line penetration consists of: | |||
(1) A closed system outside containment. | |||
(2) A containment isolation valve outside containment in each of the two lines after the penetrating line branches in the RHR sump valve room. Both of these valves are remotely controlled from the main control room. | |||
Containment Isolation Systems 6.2.4-13 | |||
The capillary sensing lines which transmit pressure from the reactor vessel to instruments in the Auxiliary Building are armored and designed to withstand DBE conditions. Any containment isolation valves installed in the RVLIS capillary lines will jeopardize the performance of the system. For this reason, isolation of these capillary lines is accomplished by a sealed sensor located inside containment and an isolator located outside containment. These devices utilize a type of bellows which transmits pressure while preventing mixing of the fluids on either side of the isolation devices. The capillary line is armored stainless steel tubing and is filled with demineralized water and sealed. A postulated shear of this capillary line on either side of the containment would not allow a leak to develop through the containment boundary.(b.2)The RCS wide range pressure transmitter (PT-68-70) is required post accident for continual indication of the pressure in the reactor vessel. The capillary sensing lines which transmit pressure from the reactor vessel to instruments in the Auxiliary Building are armored and designed to withstand DBE conditions. Any containment isolation valves installed in the RCS wide range pressure transmitter capillary lines will jeopardize the performance of the system. For this reason, isolation of these capillary lines is accomplished by a sealed sensor located inside containment and an isolator located outside containment. These devices utilize a type of bellows which transmits pressure while preventing mixing of the fluids on either side of the steel tubing and is filled and sealed. A postulated shear of this capillary line on either side of the containment would not allow a leak to develop through the containment boundary.(c)Containment isolation for each RHR sump line penetration consists of: | |||
(1)A closed system outside containment. | |||
(2)A containment isolation valve outside containment in each of the two lines after the penetrating line branches in the RHR sump valve room. Both of these valves are remotely controlled from the | |||
WATTS BAR WBNP-112 An enclosure of the RHR sump lines and isolation valves is provided from the containment out to and including the isolation valves. | |||
However, this enclosure is not designed to be leaktight after an accident for the following reasons: | |||
(1)The maximum pressure which will be experienced inside the RHR sump line will only be about 25 psig. | (1) The maximum pressure which will be experienced inside the RHR sump line will only be about 25 psig. | ||
(2)One of the isolation valves, the containment sump valve, is qualified to 600 psig. The other isolation valve, the containment spray valve, is qualified to 200 psig. | (2) One of the isolation valves, the containment sump valve, is qualified to 600 psig. The other isolation valve, the containment spray valve, is qualified to 200 psig. | ||
(3)This portion of the system only operates post accident and, therefore, only a limited leak passive failure need be postulated (and this would be at the valve). However, based on the above two statements and the fact that deadweight loading (i.e., normal operation) should not exceed the MELB criteria, the over-design should preclude any problem.Thus, the penetration has such overconservatism in its design that an external leaktight enclosure around the valves is not necessary.(d)The pressure boundary valve leak rate test line containment isolation valves (63-158, 63-112, 63-111, 63-167, 63-174, 63-21, and 63-121) are remote manually actuated from the main control room and do not receive a containment isolation signal. These valves are open for short periods of time during normal operation for the performance of SIS and RHR system venting. Thus, these valves do not automatically close when the containment isolation or safety injection signal is initiated during the venting of the SIS and RHR system. This exception is acceptable because administrative controls exist in the test document to assure valve closure after testing and containment integrity is not compromised during pump operation (i.e., during testing at accident conditions) since flow is being maintained into containment.(e)The design configuration for penetrations X-79A (ice blowing), and X-79B (negative return) is temporarily modified in operating Modes 5 and 6 and when the reactor is defueled to support ice blowing activities. | (3) This portion of the system only operates post accident and, therefore, only a limited leak passive failure need be postulated (and this would be at the valve). However, based on the above two statements and the fact that deadweight loading (i.e., normal operation) should not exceed the MELB criteria, the over-design should preclude any problem. | ||
Thus, the penetration has such overconservatism in its design that an external leaktight enclosure around the valves is not necessary. | |||
(d) The pressure boundary valve leak rate test line containment isolation valves (63-158, 63-112, 63-111, 63-167, 63-174, 63-21, and 63-121) are remote manually actuated from the main control room and do not receive a containment isolation signal. These valves are open for short periods of time during normal operation for the performance of SIS and RHR system venting. Thus, these valves do not automatically close when the containment isolation or safety injection signal is initiated during the venting of the SIS and RHR system. This exception is acceptable because administrative controls exist in the test document to assure valve closure after testing and containment integrity is not compromised during pump operation (i.e., during testing at accident conditions) since flow is being maintained into containment. | |||
(e) The design configuration for penetrations X-79A (ice blowing), and X-79B (negative return) is temporarily modified in operating Modes 5 and 6 and when the reactor is defueled to support ice blowing activities. | |||
The normally closed blind flange on each penetration will be opened and temporary piping will be installed in the penetrations. A 12-inch silicone seal will be installed between the piping segment and the penetration. Manual isolation valves will be connected to the piping on the inboard and outboard side of the penetrations. Administrative controls will ensure timely closure of the valves, if necessary, subsequent to a LOCA in the other unit. The penetrations will be returned to their normal design configuration prior to entry into Mode 4 operations. | The normally closed blind flange on each penetration will be opened and temporary piping will be installed in the penetrations. A 12-inch silicone seal will be installed between the piping segment and the penetration. Manual isolation valves will be connected to the piping on the inboard and outboard side of the penetrations. Administrative controls will ensure timely closure of the valves, if necessary, subsequent to a LOCA in the other unit. The penetrations will be returned to their normal design configuration prior to entry into Mode 4 operations. | ||
6.2.4-14 Containment Isolation Systems | |||
(1)Equipment hatch Shield Building sleeve leak (see Figure 6.2.4-12). | |||
(2)Annulus access door leak. | WATTS BAR WBNP-112 6.2.4.3.1 Possible Leakage Paths Possible leakage paths from the containment are defined below. The leakage paths are defined on the basis that the annulus pressure is less than outdoor ambient, the Auxiliary Building, and the containment pressures. Therefore, whenever containment is required, leakage is into the annulus. The possible leakage paths considered do not include containment leakage through the steel plates or through the full penetration welds in the containment vessels. The possible leakage paths also do not include Shield Building embedments. This is acceptable, as leakage through any of these paths will be into the annulus and the leakage will be processed by the EGTS. | ||
(3)Containment purge supply and exhaust isolation valves outside Shield Building leak. The possible leakage is through the valves and the leakoff (see Figure 6.2.3-2) into the annulus. | The more probable sources of containment and Shield Building leakage, such as elastomer seals, bellows, and through lines are considered as possible leak path types. Each penetration that contains elastomer seals or a bellows has at least one leakage path defined in Table 6.2.4-1. Penetrations not open to the annulus are considered as possible paths for through-line containment leakage and have one or more isolation valves. Thus every pipe penetration has at least one type of leak path listed in Table 6.2.4-1. The five different types of possible leakage paths are shown in Figure 6.2.4-20, tabulated in Table 6.2.4-1 and are discussed separately below. | ||
(4)Shield Building penetration seal leakage.Type B - Leakage | Type A - Leakage Path Type A leakage is leakage from the Auxiliary Building into the annulus. Type A penetration leakage includes the following: | ||
(1)Equipment hatch double O-ring through-line leak (see Figure 6.2.4-12). | (1) Equipment hatch Shield Building sleeve leak (see Figure 6.2.4-12). | ||
(2)Ice blowing line O-ring and blind flange through line leak (see Figures 6.2.4-16 and 6.2.4-23). | (2) Annulus access door leak. | ||
(3)Penetration bellows leak. | (3) Containment purge supply and exhaust isolation valves outside Shield Building leak. The possible leakage is through the valves and the leakoff (see Figure 6.2.3-2) into the annulus. | ||
(4)Containment purge supply and exhaust inboard and outboard valves through line leak. The leakage will pass through the leak off (see Figure 6.2.3-2) into the annulus. | (4) Shield Building penetration seal leakage. | ||
6.2.4- | Type B - Leakage Path Type B leakage paths are from the containment to the annulus. Type B leakage includes the following: | ||
(1)Shield Building Incore Instrumentation Thimble Assembly renewal line through-line leak. | (1) Equipment hatch double O-ring through-line leak (see Figure 6.2.4-12). | ||
(2)Main steam and feedwater lines annulus seal leak. | (2) Ice blowing line O-ring and blind flange through line leak (see Figures 6.2.4-16 and 6.2.4-23). | ||
(3)Ice blowing line Shield Building blind flange leak (See Figure 6.2.4-16).Type D - Leakage | (3) Penetration bellows leak. | ||
(1)Portions of the Auxiliary Building are maintained at a negative pressure relative to the outside atmosphere for the duration of an accident. Section 6.2.3 describes the implementing system and its operation. | (4) Containment purge supply and exhaust inboard and outboard valves through line leak. The leakage will pass through the leak off (see Figure 6.2.3-2) into the annulus. | ||
(2)Leakoff lines to the secondary containment and a third outboard valve receiving an isolation signal are used in certain lines (such as the containment purge lines) to prevent bypass leakage. | Containment Isolation Systems 6.2.4-15 | ||
WATTS BAR WBNP-112 (5) Containment Incore Instrumentation Thimble Assembly renewal line double O-ring through-line leak (see Figure 6.2.4-15). | |||
Type C - Leakage Path Type C leakage is leakage from the out-of-doors into the annulus and includes the following: | |||
(1) Shield Building Incore Instrumentation Thimble Assembly renewal line through-line leak. | |||
(2) Main steam and feedwater lines annulus seal leak. | |||
(3) Ice blowing line Shield Building blind flange leak (See Figure 6.2.4-16). | |||
Type D - Leakage Path Type D leakage path covers the through-line leakage from the containment to the Auxiliary Building (see Table 6.2.4-2). Included in this type of leakage are the lines associated with the safety systems required for post-LOCA operation, such as containment spray, RHR spray, high-head SIS, low-head SIS, SIS pump discharge, charging pump discharge, and containment emergency sump. For "closed" systems inside the Auxiliary Building, the through-line leakage will stay within the closed system. The component cooling water system is basically a closed system, except for the vent header at the surge tank. Any through-line leakage into the Auxiliary Building through this vent will be processed by the auxiliary building gas treatment system. | |||
Radiation monitoring is provided as a signal to initiate the closing of the vent. The nitrogen supply lines to the pressurizer relief tank and to the accumulators are normally closed. The high pressure outside of the isolation valves serves to minimize through-line leakage outward. The personnel lock is yet another possible source for through-line leakage, but the leakage through the double O-ring (assuming one door open) is small, if any, and will be processed by the auxiliary building gas treatment system. | |||
Type E - Leakage Path Type E leakage paths are paths from the containment that bypass the annulus and leak directly past a cleanup system. These leakage paths were considered during the design of the Watts Bar Nuclear Plant. The design features utilized at Watts Bar eliminates type E leakage paths. This is done by the following methods: | |||
(1) Portions of the Auxiliary Building are maintained at a negative pressure relative to the outside atmosphere for the duration of an accident. Section 6.2.3 describes the implementing system and its operation. | |||
(2) Leakoff lines to the secondary containment and a third outboard valve receiving an isolation signal are used in certain lines (such as the containment purge lines) to prevent bypass leakage. | |||
6.2.4-16 Containment Isolation Systems | |||
WATTS BAR WBNP-112 (3) A water seal(s) at greater than peak accident pressure or which has been shown by analysis to provide the necessary containment integrity is used to prevent bypass leakage in certain lines (such as the safety injection pump discharge or ERCW upper and lower compartment supply and return lines). | |||
The seals are available for at least 30 days after a design basis event (see Table 6.2.6-3. | The seals are available for at least 30 days after a design basis event (see Table 6.2.6-3. | ||
(4)The secondary side of the steam generator is kept at a higher pressure than the primary side soon after the LOCA occurs (see Section 10.4.3). Leakage between the primary and secondary sides of the steam generator is thus directed inward to the containment. | (4) The secondary side of the steam generator is kept at a higher pressure than the primary side soon after the LOCA occurs (see Section 10.4.3). Leakage between the primary and secondary sides of the steam generator is thus directed inward to the containment. | ||
(5)For the maintenance ports through penetrations X-108 and X-109, a blind flange with a double O-ring design that is not opened during power operation and has a zero leakage acceptance criteria is relied upon to prevent bypass leakage.Table 6.2.4-3 lists potential bypass leakage paths to the atmosphere and the methods chosen to eliminate such leakage.6.2.4.4 | (5) For the maintenance ports through penetrations X-108 and X-109, a blind flange with a double O-ring design that is not opened during power operation and has a zero leakage acceptance criteria is relied upon to prevent bypass leakage. | ||
6.2.4- | Table 6.2.4-3 lists potential bypass leakage paths to the atmosphere and the methods chosen to eliminate such leakage. | ||
6.2.4.4 Tests and Inspections Components of the containment isolation systems were designed, fabricated, and tested under quality assurance requirements in accordance with 10 CFR 50, Appendix B, as further described in Chapter 17. An alternative to visual examination during ASME Section III hydrostatic pressure testing was approved by Reference [1] for penetrations having inaccessible vendor welds. | |||
Nondestructive examination was performed on the components of the system in accordance with the applicable codes described in Section 3.2. | |||
Subsequent to initial plant operation, containment isolation systems are periodically tested under conditions of normal operation to determine that all systems are in constant readiness to perform the desired function. | |||
Automatic isolation valves that receive a containment isolation signal to close, where closure of the valve will not limit or restrict normal plant operation, are periodically functionally tested by the on-line testing capability described in Section 7.3.1.1.3. | |||
Other valves are periodically tested for CIS circuit electrical continuity. Other testing information is provided in Section 6.2.6. | |||
REFERENCES (1) NRC Inspection Report Nos. 50-390/90-04 and 50-391/90-04, dated May 17, 1990. | |||
Containment Isolation Systems 6.2.4-17 | |||
WATTS BAR WBNP-112 Table 6.2.4-1 Watts Bar Nuclear Plant Containment Penetrations And Barriers DUE TO THE SIZE OF TABLE 6.2.4-1 IT IS LOCATED IN THE OVERSIZED TABLE FILE 6.2.4-18 Containment Isolation Systems | |||
Containment Isolation Systems WATTS BAR Table 6.2.4-1 Watts Bar Nuclear Plant Containment Penetrations And Barriers (Sheet 65 of 69) | |||
ABBREVIATIONS FOR TABLE VALVE TYPE ACTUATORS ISOLATION SIGNAL GL = GLOBE AO = AIR OPERATED CV = CONTAINMENT VENT ISOLATION GA = GATE MO = MOTOR OPERATED PA = PHASE A BF = BUTTERFLY SO = SOLENOID OPERATED PB = PHASE B CK = CHECK M = MANUAL PR = PUMP RUN A = ANGLE CP = CONTAINMENT PRESSURE ILRT RV = RELIEF SI = SAFETY INFECTION C = CLOSED DI = DIAPHRAGM AFIS = AUXILIARY FEEDWATER ISOLATION O = OPEN SIGNAL BL = BLIND FLANGE MS = MAIN STEAM ISOLATION SIGNAL TC = TEST CONNECTION FW = FEEDWATER ISOLATION SIGNAL TO = TEST DRAIN TV = TEST VENT WV = WAFER VALVE D = DOOR BA = BALL PG = PLUG 6.2.4-19 WBNP-112 | |||
6.2.4-20 WATTS BAR Table 6.2.4-1 Watts Bar Nuclear Plant Containment Penetrations And Barriers (Sheet 66 of 69) | |||
ABBREVIATIONS FOR TABLE ACTUATION MODE VALVE POSITIONS RM = REMOTE MANUAL O = OPEN LM = LOCAL MANUAL C = CLOSED SA = SELF ACTUATOR V = VARIES AT = AUTO TRIP AI = AS IS AO = AUTO OPEN LC = LOCKED CLOSED PROCESS FLUID STATE POSSIBLE LEAKAGE PATHS C = COLD SEE FSAR SECTION 6.2.4.3.1 H = HOT FLUID BUILDING STRUCTURES A = AIR CB = CONTAINMENT BUILDING Containment Isolation Systems W = WATER SB = SHIELD BUILDING S = STEAM AB = AUXILIARY BUILDING N = NITROGEN AEB = ADDITIONAL EQUIPMENT BUILDING WBNP-112 I = ICE G = GLYCOL | |||
A | Containment Isolation Systems WATTS BAR Table 6.2.4-1 Watts Bar Nuclear Plant Containment Penetrations And Barriers (Sheet 67 of 69) | ||
: 1. A DASH IS PRINTED IN DATA SPACES THAT DO NOT APPLY TO THE PENETRATION BEING DESCRIBED. | |||
: 2. AN M AT THE END OF A CONTAINMENT OR SHIELD BUILDING PENETRATION NUMBER INDICATES THE PENETRATION HAS MORE THAN ONE LINE GOING THROUGH IT. | |||
: 3. PIPING SYSTEMS ISOLATED BY A CONTAINMENT VENTILATION (CV) SIGNAL ARE ALSO ISOLATED BY A PHASE A SIGNAL. | |||
: 4. PIPING INSIDE THE CONTAINMENT VESSEL HAS FIVE BRANCHES. IDENTICAL ISOLATION VALVES ARE INSTALLED IN EACH BRANCH. ONE VALVE IS NORMALLY OPEN. THREE OTHER VALVES ARE NORMALLY CLOSED AND ALSO RECEIVE PHASE A SIGNAL. | |||
THE FIFTH VALVE IS A RELIEF VALVE WHICH RELIEVES INTO CONTAINMENT. | |||
: 5. THE PIPING IS JOINED BY A LINE LEADING TO THE NITROGEN SUPPLY OUTSIDE OF THE SHIELD BUILDING. THIS LINE IS ISOLATED BY AN AIR OPERATED GATE VALVE WITH PHASE A ISOLATION. | |||
: 6. DUCTING OUTSIDE THE SHIELD BUILDING HAS TWO BRANCHES. IDENTICAL SECONDARY CONTAINMENT ISOLATION VALVES ARE INSTALLED IN EACH BRANCH. | |||
: 7. PIPING OUTSIDE OF THE SHIELD BUILDING HAS NINE BRANCHES. EACH LINE IS ISOLATED BY A RELIEF VALVE. | |||
: 8. INSIDE THE CONTAINMENT VESSEL A LINE IS PROVIDED FOR PRESSURE RELIEF OF THE VOLUME BETWEEN THE ISOLATION VALVES. THIS LINE IS ISOLATED BY A CHECK VALVE. | |||
: 9. THE PIPING IS JOINED BY A LINE USED FOR S.I.S. TESTING OUTSIDE OF THE SHIELD BUILDING. THIS LINE IS ISOLATED BY AN AIR OPERATED GLOBE VALVE WITH REMOTE MANUAL ACTUATION FROM THE MAIN CONTROL ROOM. | |||
: 10. THE PIPING HAS A BYPASS LINE ATTACHED TO IT INSIDE THE ANNULUS. THIS BYPASS LINE IS ISOLATED BY A LOCKED CLOSED GATE VALVE WITH LOCAL MANUAL OPERATION. | |||
: 11. ISOLATION INSIDE CONTAINMENT IS ACCOMPLISHED BY A CLOSED SYSTEM. | |||
: 12. THE DP SENSORS ARE CLOSED SYSTEMS OUTSIDE OF CONTAINMENT THAT ARE ATTACHED DIRECTLY TO THE CONTAINMENT. | |||
NO IN LINE ISOLATION VALVES ARE EMPLOYED FOR THESE SENSORS REFER TO SECTION 6.2.4.3. | |||
6.2.4-21 WBNP-112 | |||
6.2.4-22 WATTS BAR Table 6.2.4-1 Watts Bar Nuclear Plant Containment Penetrations And Barriers (Sheet 68 of 69) | |||
: 13. POST ACCIDENT MONITORING SYSTEM (PAMS) WIDE RANGE PRESSURE SENSORS ALSO MONITOR PRESSURE THROUGH THIS PENETRATION. | |||
: 14. THE SECONDARY CONTAINMENT ISOLATION VALVE(S), WHICH REPRESENT AN ADDITIONAL BOUNDARY OUTSIDE CONTAINMENT IN HVAC SYSTEMS, ARE USED TO PREVENT BYPASS LEAKAGE FROM THE ANNULUS. | |||
: 15. ISOLATION VALVES CAN BE MANUALLY ACTUATED ELECTRICALLY OR PNEUMATICALLY. | |||
: 16. THE PRIMARY AND SECONDARY CONTAINMENT PENETRATIONS ARE NOT CONNECTED EXCEPT FOR THE TYPE A TEST PRESSURIZATION. | |||
: 17. OUTSIDE CONTAINMENT, RELIEF VALVES RELEASE INTO THIS LINE IN THE EVENT OF SIS OVERPRESSURE, THUS THE SYSTEM IS ALMOST ALWAYS CLOSED, BUT COULD OPEN FOR PRESSURE RELIEF ANYTIME SIS IS ON. | |||
: 18. OUTSIDE CONTAINMENT, A ONE INCH LINE TIES IN BETWEEN THE OUTER ISOLATION VALVE AND PRIMARY CONTAINMENT. THIS LINE IS ISOLATED BY A MANUALLY LOCKED CLOSED CONTAINMENT ISOLATION VALVE. | |||
: 19. THE CONTAINMENT ISOLATION VALVES IN THIS LINE REQUIRE SIMULTANEOUS OPEN SIGNALS FROM TWO SEPARATE SWITCHES IN ORDER TO OPEN. ONE SWITCH IS LOCATED IN THE MAIN CONTROL ROOM AND THE OTHER IS LOCATED IN THE REMOTE SAMPLING STATION. | |||
: 20. DELETED FOR UNIT 2. | |||
: 21. THIS LINE TRANSMITS PRESSURE FROM THE PRIMARY COOLANT SYSTEM TO PRESSURE INSTRUMENTATION FOR DETERMINING THE REACTOR VESSEL FLUID LEVEL. THE LINE IS FLUID FILLED AND DOUBLE DIAPHRAGMED TO PREVENT COMMUNICATION BETWEEN THE PRIMARY SYSTEM FLUID AND THE AUXILIARY BUILDING. NO PRIMARY SYSTEM FLUID TRAVELS THROUGH THE Containment Isolation Systems PENETRATION SINCE THE INNER DIAPHRAGM IS LOCATED NEAR THE REACTOR VESSEL. SINCE DOUBLE DIAPHRAGMS ARE EMPLOYED FOR CONTAINMENT ISOLATION, NO CONTAINMENT ISOLATION VALVES ARE USED. | |||
: 22. THIS LINE JOINS THE SECONDARY SIDE OF THE STEAM GENERATOR(S) INSIDE CONTAINMENT AND IS THEREFORE CONSIDERED A CLOSED SYSTEM INSIDE CONTAINMENT. THE ISOLATION VALVES WHICH EXIST OUTBOARD OF CONTAINMENT ARE NOT LEAKRATE TESTED DUE TO FLOODING OF THE STEAM GENERATORS POST LOCA. | |||
WBNP-112 | |||
Containment Isolation Systems WATTS BAR Table 6.2.4-1 Watts Bar Nuclear Plant Containment Penetrations And Barriers (Sheet 69 of 69) | |||
: 23. BETWEEN PRIMARY CONTAINMENT AND THE OUTER ISOLATION VALVE IN THIS LINE, AN AUXILIARY FEEDWATER LINE ADJOINS. | |||
THE AUXILIARY FEEDWATER LINE HAS ISOLATION VALVES WHICH ARE ISOLATED IN THE SAME MANNER AS THE AUXILIARY FEEDWATER ISOLATION VALVES LISTED FOR X-40A AND X-40B. | |||
: 24. NOT USED | |||
: 25. AZIMUTH INFORMATION FOR THESE LINES CAN BE FOUND IN CHICAGO BRIDGE & IRON CO. STEEL CONTAINMENT VESSEL DATA PACKAGE (RIMS #B48850425301). | |||
: 26. NO TYPE C LEAKAGE RATE TEST IS PERFORMED ON THIS LINE, BUT A WATER INVENTORY LEAKAGE RATE TEST IS PERFORMED ON THE MOV LOCATED OUTSIDE CONTAINMENT. THIS WATER LEAKAGE TEST ASSURES THAT THE WATER LEG, LOCATED IMMEDIATELY INBOARD OF THE MOV, WILL MAINTAIN A SUFFICIENT INVENTORY TO MAINTAIN A PRESSURE OF AT LEAST 1.1 TIMES THE MAXIMUM CALCULATED CONTAINMENT ACCIDENT PRESSURE ON THE MOV FOR 30 DAYS AFTER AN ACCIDENT. | |||
: 27. PENETRATION X-118 IS OPENED BY REMOVING THE BLIND FLANGE IN THE ANNULUS TO ALLOW THE WATER WHICH HAS COLLECTED IN THE ANNULUS FROM LEAKAGE THROUGH THE PENETRATIONS OR SEEPAGE THROUGH THE CONCRETE TO DRAIN THE REACTOR BUILDING FLOOR AND EQUIPMENT DRAIN SUMP. | |||
: 28. THIS LINE TRANSMITS PRESSURE FROM THE PRIMARY COOLANT SYSTEM TO PRESSURE INSTRUMENTATION. THE LINE IS FLUID FILLED AND DOUBLE DIAPHRAGMED TO PREVENT COMMUNICATION BETWEEN THE PRIMARY SYSTEM FLUID AND THE AUXILIARY BUILDING. NO PRIMARY SYSTEM FLUID TRAVELS THROUGH THE PENETRATION SINCE THE INNER DIAPHRAGM IS LOCATED NEAR THE REACTOR VESSEL. SINCE DOUBLE DIAPHRAGMS ARE EMPLOYED FOR CONTAINMENT ISOLATION, NO CONTAINMENT ISOLATION VALVES ARE USED. | |||
: 29. SYS.26 HPFP LINE SUPPLIES THE CABLE TRAY INTERACTION (RB ANNULUS) THROUGH SHIELD BUILDING PEN. MK 103 LOCATED AT THE SAME EL AND AZ AS CONTAINMENT PEN.X-88 (REF.DWG. 47W850-9). | |||
: 30. SYS.26 HPFP LINE SUPPLIES THE STAND PIPE (RB ANNULUS) THROUGH SHIELD BUILDING PEN. MK 104 LOCATED AT THE SAME EL AND AZ AS CONTAINMENT PEN.X-89 (REF.DWG. 47W850-9). | |||
6.2.4-23 WBNP-112 | |||
Table 6.2.4-2 Possible Bypass Leakage Paths To The Auxiliary Building (Page 1 of 6) 6.2.4-24 WATTS BAR Penetration Number Penetrating Line Name Description X-2 A, B Personnel Access Hatch Any leakage would be treated by the ABGTS. | |||
X-3 Fuel Transfer Tube Any leakage would be treated by the ABGTS. | |||
X-15 Chemical and Volume Letdown Line Any leakage would be treated by the ABGTS. | |||
X-16* Normal Charging Line High water pressure maintained on outboard valve, even in the event of a single failure. | |||
X-17 RHR Hot Leg Injection System is in operation after an accident. Cross ties between pumps maintain flows in the event of a single failure. | |||
X-19 A&B* RHR Sump Suction Line Line is always filled with water. No atmospheric bypass leakage to the Auxiliary Building can occur after a LOCA. | |||
X-20 A&B* SIS RHR Pump Discharge System is in operation after a LOCA. Cross ties between pumps maintain flows and pressure in the event of a single failure. | |||
X-21* Safety Injection Pump Discharge Line in use during a LOCA which will be pressurized even in the event of a single failure due to cross ties between pumps. | |||
X-22* Charging Pump Discharge Same as for Penetration No. 21. | |||
X-24* SIS Relief Valve Discharge Any leakage through the relief valve is prevented as the valves are pressurized Containment Isolation Systems outside containment by the SIS system. Any leakage would be into containment. | |||
X-25A Pressurizer Liquid Sample Any leakage would be treated by the ABGTS. | |||
X-25D Pressurizer Steam Sample Any leakage would be treated by the ABGTS. | |||
WBNP-112 X-27 A, B, C, D Steam Generator Sample Lines Any leakage would be treated by the ABGTS. | |||
Table 6.2.4-2 Possible Bypass Leakage Paths To The Auxiliary Building (Page 2 of 6) | |||
Containment Isolation Systems WATTS BAR Penetration Number Penetrating Line Name Description X-29 CCS from RC Pump Coolers Any leakage would be treated by the ABGTS. | |||
X-30 Accumulator to Holdup Tanks Any leakage would be treated by the ABGTS. | |||
X-31 Fire Protection Any leakage would be treated by the ABGTS. | |||
X-32* Safety Injection Discharge Same as for Penetration No. 21. | |||
X-33* Safety Injection Discharge Same as for Penetration No. 21. | |||
Penetration | X-34 Control Air I&C Any leakage would be treated by the ABGTS. | ||
X-35 CCS from Excess Letdown Heat Exchanger Same as for Penetration No. 29. | |||
Any leakage would be treated by the ABGTS. | X-39A N2 to Accumulators Any leakage would be treated by the ABGTS. | ||
X-39B N2 to Pressurizer Relief Tank Any leakage would be treated by the ABGTS. | |||
X-40D Service Air Any leakage would be treated by the ABGTS. | |||
X-44 X-45 X-46 X-47A X- | X-41 Floor Sump Pump Discharge Any leakage would be treated by the ABGTS. | ||
X-42 Pressurizer Relief Tank Makeup Any leakage would be treated by the ABGTS. | |||
X-43 A*,B*,C*,D* To RC Pump Seals The line is pressurized during a LOCA even in the event of a single failure. If there was any leakage it would be treated by the ABGTS. | |||
X-44 From RC Pump Seals Any leakage would be treated by the ABGTS. | |||
X-45 RC Drain Tank and PRT to Vent Header Any leakage would be treated by the ABGTS. | |||
X-46 RC Drain Tank Pump Discharge Any leakage would be treated by the ABGTS. | |||
X-47A Glycol Line to Ice Condenser Any leakage would be treated by the ABGTS. | |||
WBNP-112 X-47B Glycol Line from Ice Condenser Any leakage would be treated by the ABGTS. | |||
6.2.4-25 | |||
Table 6.2.4-2 Possible Bypass Leakage Paths To The Auxiliary Building (Page 3 of 6) 6.2.4-26 WATTS BAR Penetration Number Penetrating Line Name Description X-48 A&B* Containment Spray System in operation after a LOCA. A 30-day water leg seal is maintained in this line. | |||
X-49 A&B RHR Spray System in operation after a LOCA. System pressure maintained even in the event of a single failure due to pump cross ties. | |||
X-50A RCP Thermal Barrier Return Same as for Penetration No. 29. | |||
X-50B RCP Thermal Barrier Supply Any leakage would be treated by the ABGTS. | |||
X-52* CCS to RC Pump Coolers Same as for Penetration No. 43. | |||
X-53* CCS to Excess Letdown Heat Exchanger Same as for Penetration No. 43. | |||
X-56A* Lower Containment ERCW Supply High water pressure maintained on outboard valve, even in the event of a single failure. | |||
X-56A*X-57A* | X-57A* Lower Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure. | ||
X-58A* | X-58A* Lower Containment ERCW Supply High water pressure maintained on outboard valve, even in the event of a single failure. | ||
X-58B X-59A*X-60A* | X-58B RCS Pressure Sensor Any leakage would be treated by the ABGTS. | ||
X-61A* | X-59A* Lower Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure. | ||
X-62A* | Containment Isolation Systems X-60A* Lower Containment ERCW Supply High water pressure maintained on outboard valve, even in the event of a single failure. | ||
X-63A* | X-61A* Lower Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure. | ||
X-62A* Lower Containment ERCW Supply High water pressure maintained on outboard valve, even in the event of a WBNP-112 single failure. | |||
X-63A* Lower Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure. | |||
Table 6.2.4-2 Possible Bypass Leakage Paths To The Auxiliary Building (Page 4 of 6) | |||
Any leakage would be treated by the ABGTS. | Containment Isolation Systems WATTS BAR Penetration Number Penetrating Line Name Description X-64 Inst. Rm, AC Chilled Water Return Any leakage would be treated by the ABGTS. | ||
High water pressure maintained on outboard valve, even in the event of a single failure.High water pressure maintained on outboard valve, even in the event of a single failure.High water pressure maintained on outboard valve, even in the event of a single failure. | X-65 Inst. Rm. AC Chilled Water Supply Any leakage would be treated by the ABGTS. | ||
X-66 Inst. Rm. AC Chilled Water Return Any leakage would be treated by the ABGTS. | |||
X-67 Inst. Rm. AC Chilled Water Supply Any leakage would be treated by the ABGTS. | |||
X-68* Upper Containment ERCW Supply High water pressure maintained on outboard valve, even in the event of a single failure. | |||
X-69* Upper Containment ERCW Supply High water pressure maintained on outboard valve, even in the event of a single failure. | |||
X-70* Upper Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure. | |||
X-71* Upper Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure. | |||
X-72* Upper Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure. | |||
X-73* Upper Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure. | |||
X-74* Upper Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure. | |||
X-75* Upper Containment ERCW Supply High water pressure maintained on outboard valve, even in the event of a single failure. | |||
X-76 Service Air Any leakage would be treated by the ABGTS. | |||
X-77 Demineralized Water Any leakage would be treated by the ABGTS. | |||
6.2.4-27 WBNP-112 X-78 Fire Protection Any leakage would be treated by the ABGTS. | |||
Table 6.2.4-2 Possible Bypass Leakage Paths To The Auxiliary Building (Page 5 of 6) 6.2.4-28 WATTS BAR Penetration Number Penetrating Line Name Description X-81 RC Drain Tank to Gas Analyzer Any leakage would be treated by the ABGTS. | |||
X-82 Refueling Cavity C-U Pump Suction Any leakage would be treated by the ABGTS. | |||
X-83 Refueling Cavity C-U Pump Discharge Any leakage would be treated by the ABGTS. | |||
Any leakage would be treated by the ABGTS.Any leakage would be treated by the ABGTS.Any leakage would be treated by the ABGTS. | X-84A Pressurizer Relief Tank to Gas Analyzer Any leakage would be treated by the ABGTS. | ||
Any leakage would be treated by the ABGTS.Any leakage would be treated by the ABGTS.Any leakage would be treated by the ABGTS. | X-84B Reactor Vessel Level Indicating System Any leakage would be treated by the ABGTS. | ||
Any leakage would be treated by the ABGTS. | X-84C Reactor Vessel Level Indicating System Any leakage would be treated by the ABGTS. | ||
X-84D Reactor Vessel Level Indicating System Any leakage would be treated by the ABGTS. | |||
X-85B Hot Leg Sample Any leakage would be treated by the ABGTS. | |||
X-87B Reactor Vessel Level Indicating System Any leakage would be treated by the ABGTS. | |||
Any leakage would be treated by the ABGTS. | X-87C Reactor Vessel Level Indicating System Any leakage would be treated by the ABGTS. | ||
X-87D Reactor Vessel Level Indicating System Any leakage would be treated by the ABGTS. | |||
X-90 Control Air Any leakage would be treated by the ABGTS. | |||
X-91 Control Air Any leakage would be treated by the ABGTS. | |||
Containment Isolation Systems WBNP-112 | |||
Table 6.2.4-2 Possible Bypass Leakage Paths To The Auxiliary Building (Page 6 of 6) | |||
Containment Isolation Systems WATTS BAR Penetration Number Penetrating Line Name Description X-93 Accumulator Sample Any leakage would be treated by the ABGTS. | |||
X-94 B, X-95 B Containment Atmosphere Radiation Monitor Any leakage would be treated by the ABGTS. | |||
X-94 C, X-95 C Containment Atmosphere Radiation Monitor Any leakage would be treated by the ABGTS. | |||
X-99 H2 Analyzer Any leakage would be treated by the ABGTS. | |||
X-100 H2 Analyzer Any leakage would be treated by the ABGTS. | |||
X-107 RHR Supply Any leakage would be treated by the ABGTS. | |||
X-114 Ice Condenser (from Glycol Floor Cooling Coils) Any leakage would be treated by the ABGTS. | |||
X-115 Ice Condenser (to Glycol Floor Cooling Coils) Any leakage would be treated by the ABGTS. | |||
* Not a bypass leakage path to the Auxiliary Building. | |||
6.2.4-29 WBNP-112 | |||
Table 6.2.4-3 Prevention Of Bypass Leakage To The Atmosphere (Page 1 of 2) 6.2.4-30 WATTS BAR Penetration Number Penetration Line Name Description X-4 Lower Compartment Purge Air Exhaust Leakoff lines to the annulus X-5 Instrument Room Purge Air Exhaust Leakoff lines to the annulus X-6 Upper Compartment Purge Air Exhaust Leakoff lines to the annulus X-7 Upper Compartment Purge Air Exhaust Leakoff lines to the annulus X-8A Feedwater Bypass Secondary side of the steam generator is pressurized above containment pressure X-8B Feedwater Bypass Same as for Penetration X-8A X-8C Feedwater Bypass Same as for Penetration X-8A X-8D Feedwater Bypass Same as for Penetration X-8A X-9A Upper Compartment Purge Air Supply Leakoff lines to the annulus X-9B Upper Compartment Purge Air Supply Leakoff lines to the annulus X-10A Lower Compartment Purge Air Supply Leakoff lines to the annulus X-10B Lower Compartment Purge Air Supply Leakoff lines to the annulus X-11 Instrument Room Purge Air Supply Leakoff lines to the annulus X-12A Feedwater Same as for Penetration X-8A X-12B Feedwater Same as for Penetration X-8A X-12C Feedwater Same as for Penetration X-8A X-12D Feedwater Same as for Penetration X-8A X-13A Main Steam Same as for Penetration X-8A X-13B Main Steam Same as for Penetration X-8A Containment Isolation Systems WBNP-112 | |||
6.2. | Table 6.2.4-3 Prevention Of Bypass Leakage To The Atmosphere (Page 2 of 2) | ||
Containment Isolation Systems WATTS BAR Penetration Number Penetration Line Name Description X-13C Main Steam Line Same as for Penetration X-8A X-13D Main Steam Line Same as for Penetration X-8A X-14A, B, C, D Steam Generator Blowdown Same as for Penetration X-8A X-40A Auxiliary Feedwater Same as for Penetration X-8A X-40B Auxiliary Feedwater Same as for Penetration X-8A X-56A Lower Compartment ERCW Supply Leakage prevented by combination of water seal and piping traps in conjunction with acceptance limits for Appendix J Testing as defined in design output. | |||
X-57A Lower Compartment ERCW Return Same as for Penetration X-56A X-58A Lower Compartment ERCW Supply Same as for Penetration X-56A X-59A Lower Compartment ERCW Return Same as for Penetration X-56A X-60A Lower Compartment ERCW Supply Same as for Penetration X-56A X-61A Lower Compartment ERCW Return Same as for Penetration X-56A X-62A Lower Compartment ERCW Supply Same as for Penetration X-56A X-63A Lower Compartment ERCW Return Same as for Penetration X-56A X-68 Upper Compartment ERCW Supply Same as for Penetration X-56A X-69 Upper Compartment ERCW Supply Same as for Penetration X-56A X-70 Upper Compartment ERCW Return Same as for Penetration X-56A X-71 Upper Compartment ERCW Return Same as for Penetration X-56A X-72 Upper Compartment ERCW Return Same as for Penetration X-56A X-73 Upper Compartment ERCW Return Same as for Penetration X-56A X-74 Upper Compartment ERCW Supply Same as for Penetration X-56A X-75 Upper Compartment ERCW Supply Same as for Penetration X-56A X-80 Lower Compartment Pressure Relief Leakoff lines to the annulus X-108 Maintenance Port Blind Flange, double O-ring design with a zero leakage criteria; not open during power operation X-109 Maintenance Port Blind flange, double O-ring design with a zero leakage criteria; not open during power WBNP-112 operation 6.2.4-31 | |||
6.2. | Table 6.2.4-4 Instrument Lines Penetrating Primary Containment (Page 1 of 3) 6.2.4-32 WATTS BAR Inner Outer Line Isolation Isolation Penetration Size Valve Valve Valve Valve Valve Valve Line Identification No. Number Inches Orifice Number Type Location Number Type Location Pressurizer Liquid 1 X-25A 3/8 No 43-11 Globe Inside Prim 43-12 Globe Annulus Sample Containment Pressurizer Steam 2 X-25D 3/8 No 43-2 Globe Inside Prim 43-3 Globe Annulus Sample Containment dP Sensor1 3 X-26C 1/2 No - - - - - - | ||
Steam Generator 4 X-27A 3/8 No 43-54D Globe Inside Prim 43-55 Globe Annulus No. 1 Sample and Water Containment Quality Steam Generator 5 X-27B 3/8 No 43-56D Globe Inside Prim 43-58 Globe Annulus No. 2 Sample Containment Steam Generator 6 X-27C 3/8 No 43-59D Globe Inside Prim 43-61 Globe Annulus No. 3 Sample Containment Steam Generator 7 X-27D 3/8 No 43-63D Globe Inside Prim 43-64 Globe Annulus No. 4 Sample Containment dP Sensor1 X-57B 1/2 No - - - - - - | |||
dP Sensor1 X-60B 1/2 No - - - - - - | |||
dP Sensor1 X-102 1/2 No - - - - - - | |||
Containment Isolation Systems WBNP-112 | |||
6.2. | Table 6.2.4-4 Instrument Lines Penetrating Primary Containment (Page 2 of 3) | ||
Containment Isolation Systems WATTS BAR Inner Outer Line Isolation Isolation Penetration Size Valve Valve Valve Valve Valve Valve Line Identification No. Number Inches Orifice Number Type Location Number Type Location Accum. to Holdup Tanks 8 X-30 3/4 No 63-071 Globe Inside Prim 63-084 Globe Outside Shield Containment Building Pressurizer Relief 9 X-84A 3/8 No 68-308 Globe Inside Prim 68-307 Globe Annulus Tank to Gas Analyzer Containment Reactor Vessel Level 10 X-84B 3/16 No - - - - - - | |||
Ind Sys Reactor Vessel Level 11 X-84C 3/16 No - - - - - - | |||
Ind Sys Reactor Vessel Level 12 X-84D 3/16 No - - - - - - | |||
Ind Sys Hot Leg Sample - Loops 13 X-85B 3/8 No 43-22 Globe Inside Prim 43-23 Globe 1 and 3 Containment Reactor Vessel Level 16 X-87B 3/16 No - - - - | |||
Ind Sys 6.2.4-33 WBNP-112 | |||
Table 6.2.4-4 Instrument Lines Penetrating Primary Containment (Page 3 of 3) 6.2.4-34 WATTS BAR Inner Outer Line Isolation Isolation Penetration Size Valve Valve Valve Valve Valve Valve Line Identification No. Number Inches Orifice Number Type Location Number Type Location Reactor Vessel Level 17 X-87C 3/16 No - - - - - - | |||
Ind Sys Reactor Vessel Level 18 X-87D 3/16 No - - - - - - | |||
Ind Sys Accumulator Sample 19 X-93 3/8 No 43-34 Globe Inside Prim Globe Annulus Containment 43-35 Lower Compartment 20 X-94B 1-1/2 No 90-110 Globe Inside Prim 90-111 Globe Annulus Air Monitor Intake Containment 90-108 90-107 Lower Compartment 21 X-94C 1-1/2 No 90-109 Globe Inside Prim Globe Annulus Air Monitor Return Containment Upper Compartment 22 X-95B 1-1/2 No 90-116 Globe Inside Prim 90-117 Globe Annulus Air Monitor Intake Containment Upper Compartment 23 X-95C 1-1/2 No 90-114 Globe Inside Prim 90-113 Globe Annulus Air Monitor Return 90-115 Containment Containment dP Sensor1 24 X-97 1/2 No - - - - - - | |||
(PdT-30-133) | |||
6.2. | Containment dP Sensor1 25 X-98 1/2 No - - - - - - | ||
(PdT-30-30C) | |||
Hydrogen Analyzer 26 X-99 3/8 No 43-202 Globe Inside Prim. 43-434 Globe Annulus Containment Isolation Systems Containment Hydrogen Analyzer 27 X-100 3/8 No 43-201 Globe Inside Prim. 43-433 Globe Annulus Containment WBNP-112 1 | |||
These have no in-line containment isolation valves - see Section 6.2.4.3 and Table 6.2.4-1. | |||
WATTS BAR Containment Isolation Systems Figure 6.2.4-1 Type 1, Main Steam X-l3A, X-l3B, X-l3C, X-13D WBNP-112 6.2.4-35 | |||
6.2.4-36 WATTS BAR Figure 6.2.4-2 Type II, Feedwater X-12A, X-l2B, X-12C, X-12D WBNP-112 Containment Isolation Systems | |||
6.2. | |||
WATTS BAR Containment Isolation Systems Figure 6.2.4-3 Type III, Residual Heat Removal Pump Return X-17, Pump Supply X-I07 WBNP-112 6.2.4-37 | |||
6.2.4-38 WATTS BAR Figure 6.2.4-4 Type IV and V (Type IV Socket Weld Ends, Type V Butt Weld Ends) | |||
WBNP-112 Containment Isolation Systems | |||
WATTS BAR Containment Isolation Systems Figure 6.2.4-5 Type VI and VII (Type VI for Socket Weld SS Process Lines, Type 6.2.4-39 VII for Butt Weld SS Process Lines) WBNP-112 | |||
WATTS BAR WBNP-112 Figure 6.2.4-6 Type VIII, for Butt Weld C.S. Process Lines 6.2.4-40 Containment Isolation Systems | |||
Control | WATTS BAR WBNP-112 Figure 6.2.4-7 Type IX, for SS Process Lines Containment Isolation Systems 6.2.4-41 | ||
WATTS BAR WBNP-112 Figure 6.2.4-8 Type X, Instrument Penetrations 6.2.4-42 Containment Isolation Systems | |||
WATTS BAR WBNP-112 Figure 6.2.4-9 Type XII, Emergency Sump Containment Isolation Systems 6.2.4-43 | |||
WATTS BAR WBNP-112 Figure 6.2.4-10 Type XI, Emergency Sump 6.2.4-44 Containment Isolation Systems | |||
WATTS BAR WBNP-112 Figure 6.2.4-11 Type XIII, Ventilation Duct Penetration Containment Isolation Systems 6.2.4-45 | |||
WATTS BAR WBNP-112 Figure 6.2.4-12 Type XIV, Equipment Hatch 6.2.4-46 Containment Isolation Systems | |||
WATTS BAR WBNP-112 Figure 6.2.4-13 Type XV, Personnel Access Containment Isolation Systems 6.2.4-47 | |||
WATTS BAR WBNP-112 Figure 6.2.4-14 Type XVI, Transfer Tube 6.2.4-48 Containment Isolation Systems | |||
WATTS BAR WBNP-112 Figure 6.2.4-15 Type XVII, Incore Instrumentation Thimble Assembly Renewal Line Containment Isolation Systems 6.2.4-49 | |||
WATTS BAR WBNP-112 Figure 6.2.4-16 Type XVIII, Ice Blowing Line 6.2.4-50 Containment Isolation Systems | |||
WATTS BAR WBNP-112 Figure 6.2.4-17 Type XIX, Electrical Penetration Containment Isolation Systems 6.2.4-51 | |||
6.2.4-52 WATTS BAR Figure 6.2.4-17A Type XX Feedwater Bypass Penetrations X-8A, X-8B, X-8C, X-8D WBNP-112 Containment Isolation Systems | |||
WATTS BAR WBNP-112 Figure 6.2.4-17B Type XXI, Upper And Lower Containment ERCW Supply And Return CCW From Excess Letdown Heat Exchanger and from Pump Odolers Containment Isolation Systems 6.2.4-53 | |||
WATTS BAR WBNP-112 Figure 6.2.4-17C Type XXII Multi Line Penetration X-39 6.2.4-54 Containment Isolation Systems | |||
WATTS BAR Containment Isolation Systems Figure 6.2.4-17D Type XXIII Instrument Room Chilled H20 Supply and Return WBNP-112 6.2.4-55 | |||
WATTS BAR WBNP-112 Figure 6.2.4-17E Type XXIV UHI X-l08, X-109 6.2.4-56 Containment Isolation Systems | |||
WATTS BAR WBNP-112 Figure 6.2.4-18 Mechanical Containment Penetration Containment Isolation Systems 6.2.4-57 | |||
6.2.4-58 WATTS BAR Figure 6.2.4-19 Powerhouse Reactor Building Unit 1 & 2 Mechanical Sleeves-Shield Building WBNP-112 Containment Isolation Systems | |||
WATTS BAR WBNP-112 Figure 6.2.4-20 Schematic Diagram of Leakage Paths Containment Isolation Systems 6.2.4-59 | |||
6.2.4-60 WATTS BAR Figure 6.2.4-21 Electrical Logic Diagram Containment Isolation WBNP-112 Containment Isolation Systems | |||
WATTS BAR WBNP-112 Figure 6.2.4-22A through 6.2.4-22II Deleted by Amendment 65 Containment Isolation Systems 6.2.4-61 | |||
6.2.4-62 WATTS BAR Figure 6.2.4-23 Ice Blowing and Negative Return Lines - Blind Flange Details WBNP-112 Containment Isolation Systems | |||
WATTS BAR WBNP-112 6.2.5 Combustible Gas Control in Containment The containment combustible gas control system is designed to control the concentration of hydrogen that may be released into the containment following a beyond-design-basis accident to ensure that containment structural integrity is maintained. The combustible gas control system consists of the containment air return system, the hydrogen analyzer system (HAS) and the hydrogen mitigation system (HMS) which conform to 10 CFR 50.44 requirements. | |||
6.2.5.1 Design Bases In an accident more severe than the design-basis loss-of-coolant accident, combustible gas is predominantly generated within containment as a result of the following: | |||
(1) Fuel clad-coolant reaction between the fuel cladding and the reactor coolant. | |||
(2) Molten core-concrete interaction in a severe core melt sequence with a failed reactor vessel. | |||
If a sufficient amount of combustible gas is generated, it may react with the oxygen present in the containment at a rate rapid enough to lead to a containment breach or a leakage rate in excess of Technical Specification limits. Additionally, damage to systems and components essential to continued control of the post-accident conditions could occur. | |||
The systems provided for combustible gas control have the following functional and mechanical requirements: | |||
(1) The air return fans enhance the ice condenser and containment spray heat removal operation by circulating air from the upper compartment to the lower compartment through the ice condenser, and then back to the upper compartment. Hydrogen concentration is limited in potentially stagnant regions by providing air flow in these regions. | |||
(2) The HAS provides the capability for extracting a sample and obtaining the measurement necessary to determine the volume percent concentration for hydrogen present in the sample. The system provides indication and alarms of volume percent concentrations in the main control room. Indication is also provided at the remote control center. | |||
(3) The HMS is designed to increase the containment capability to accommodate hydrogen that could be released during a degraged core accident. The system is based on the concept of controlled ignition using thermal igniters. | |||
(4) The air return fans and HAS are designed to operate continuously during accident conditions. The HMS igniter assemblies are qualified for a 30 year life of operational cycles. | |||
Combustible Gas Control in Containment 6.2.5-1 | |||
WATTS BAR WBNP-112 (5) The combustible gas control system is designed for periodic testing and inspection. | |||
6.2.5.2 System Design Containment Air Return System Mixing of the containment atmosphere is accomplished by the containment air return system described in Section 6.8. The air return fans start automatically 9 + 1 minutes after receipt of a containment Phase B isolation signal (see 7.3.1.1.1). In addition, the fans may be started manually. | |||
The associated ductwork, which must remain intact following a beyond-design-basis accident to assure that no localized hydrogen concentration exceeds 4%, consists of (1) two 12-inch ducts (one associated with each air return fan intake) which draw air from the containment dome region, (2) one 8-inch duct which circles the containment removing air from accumulator rooms and other dead-ended spaces and terminates at each air return fan housing, (3) two 12-inch ducts which circle the crane wall, removing air from the steam generator and pressurizer compartments and terminate through two 8-inch ducts at each air return fan housing, (4) two 8-inch pipes (one connected to each air return fan housing) which remove air from the refueling canal, and (5) the main duct between upper and lower compartment through the divider deck, including the non-return dampers. | |||
The ductwork described above is embedded in concrete, where possible, to prevent damage from buildup of pressure during a beyond-design-basis accident. Ductwork not protected by embedment is also designed to withstand the beyond-design-basis accident environment. The air return system also includes heavy-duty backdraft dampers to prevent back flow from the lower compartment to the upper compartment under a differential pressure of 15 psig. These dampers prevent steam from bypassing the ice condenser during the initial blowdown. Figures 6.2.5-3, 6.2.5-4 and 6.2.5-5 are provided to show the routing of the recirculation ducts. | |||
During the post-blowdown period, the pressure gradient between containment compartments is almost nonexistent and hydrogen can accumulate in potentially stagnant regions. The regions of concern are the ten dead-ended compartments: the four steam generator enclosures; the pressurizer enclosure; the four accumulator spaces; and the instrument room. The air return fans provide recirculation flow through the dead-ended compartments to prevent excessive hydrogen buildup. Each fan will mix 1,960 cfm form the enclosed areas in the lower compartment to the general lower compartment atmosphere. | |||
Hydrogen Analyzer The HAS provides the capability to extract air samples from containment and to determine volume percent concentration of hydrogen. The primary functions of the system include continuous sampling from a remote location, measurement of hydrogen partial pressure, visual indication of volume percent concentrations and hydrogen concentration alarms in the main control room. | |||
6.2.5-2 Combustible Gas Control in Containment | |||
WATTS BAR WBNP-112 The sampling system consists of a single, non-trained detection loop. The analyzer is fed by one process sample line and returns to containment on one process effluent line. This line is equipped with two manually controlled isolation valves on both the sample and return lines. The system is installed at two locations. The sample loop station, mounted inside the Annulus, consists of the detection chamber, pressure transducer, solenoid valves, condensate management components and check valves for directing sample through the loop. | |||
The HAS remote control center is mounted is a mild environment in the Auxiliary Building where access is always permitted. The major components of the center include a PLC based signal conditioner/system controller, a remote touch screen display and the system switch panel. | |||
Containment isolation valve hand switches, a fan control hand switch, a hydrogen concentration indicator and alarms are provided in the main control room. | |||
Upon actuation of the system, sample enters the loop assembly and passes through a T which separates the liquid and collects it in a condensate trap. The sample continues through a flow switch into the detection chamber. Inside the detection chamber, partial and total pressure measurements are obtained. The sample exits the detection chamber, passing through the sample pump which then drives the sample out of the loop assembly. | |||
The analyzer is designed to continually measure hydrogen concentration following a beyond-design-basis accident. The analyzer is calibrated to measure hydrogen concentrations between zero and ten percent with an accuracy of +0.2% hydrogen. A sample loop flow diagram is shown in Figure 6.2.5-6. | |||
The hydrogen analyzer components are seismically supported. | |||
Hydrogen Mitigation System To assure that any hydrogen release would be ignited at containment locations as soon as the concentration exceeded the lower flammability limit, durable thermal igniters, capable of maintaining an adequate surface temperature, are used. An igniter developed by Tayco Engineering, operating at a nominal plant voltage of 120V AC, is used. The igniter has been shown by experiment to be capable of maintaining surface temperatures in excess of the required minimum for extended periods, initiating combustion and continuing to operate in various combustion environments. | |||
The igniters in the HMS are equally divided into two redundant groups, each with independent and separate controls, power supplies and locations, to ensure adequate coverage even in the event of a single failure. Manual control of each group of igniters is provided in the main control room and the status (on-off) of each group is indicated there. A separate train of Class IE 480V AC auxiliary power is provided for each group of igniters and is backed by automatic loading onto the diesel generators upon loss of offsite power. Each individual circuit powers two igniters. See Figures 6.2.5-8 through 6.2.5-12 for igniter locations. | |||
Combustible Gas Control in Containment 6.2.5-3 | |||
WATTS BAR WBNP-112 To assure adequate spatial coverage, 68 igniters are distributed throughout the various regions of the containment in which hydrogen could be released or to which it could flow in significant quantities (see Figures 6.2.5-8 through 6.2.5-12). There are at least two igniters, controlled and powered redundantly located in each of these regions. Following a degraded core accident, any hydrogen which is produced is released into the lower compartment inside the crane wall. To cover this region, 22 igniters (equally divided between trains) are provided. Eight of these are distributed on the reactor cavity wall exterior and crane wall interior at an intermediate elevation to ensure the partial burning that accompanies upward flame propagation. | |||
Two igniters are located at the lower edge of each of the five enclosures for the four steam generators and the pressurizer, two in the top of the pressurizer enclosure and another pair above the reactor vessel in the cavity. These 22 lower compartment igniters help prevent flammable mixtures from entering the ice condenser. Any hydrogen not burned in the lower compartment is carried up through the ice condenser and into its upper plenum. Since steam is removed from the mixture as it is passed through the ice bed, mixtures that were nonflammable in the lower compartment tend to be flammable in the ice condenser upper plenum. This phenomenon is supported by the CLASIX containment analysis code which predicts more sequential burns to occur in the upper plenum than in any other region. Four igniters are located around the upper compartment dome, four at intermediate elevations on the outside of the steam generator enclosures, four more around the top inside of the crane wall and on above each of the two air return fans. The air return fans provide recirculation flow from the upper compartment through several dead-ended compartments (see Section 6.2.1.3.3) back into the main part of the lower compartment. To cover this region, there are pairs of igniters in each of the eight rooms (a total of 16 igniters) through which the recirculation flow passes. The location of the HMS igniters is shown in Figures 6.2.5-8 through 6.2.5-12. | |||
The components of the HMS inside containment are seismically supported. | |||
6.2.5.3 Design Evaluation Containment pressure during the post blowdown phase of a loss-of-coolant accident is calculated with the LOTIC code which models the containment structural heat sinks and containment safeguards system. The long-term containment pressure analysis accounts for hydrogen partial pressure. This transient is discussed in Section 6.2.1 and 15.4.1.2. | |||
The containment air return system is designed to reduce containment pressure after blowdown to prevent excessive hydrogen concentrations in pocketed areas, and circulate air through the ice condenser. The air return fans automatically start on a Phase B containment isolation signal and can be started manually. The fans provide a continuous mixing of the containment compartment atmosphere for the long-term post-blowdown environment. The system has redundancy, is single-failure-proof and will remain operable with a loss of onsite or offsite power. | |||
The hydrogen analyzer is a highly reliable commerical grade, Category 3 instrument as defined in Regulatory Guide 1.97 and permitted by Regulatory Guide 1.7. The 6.2.5-4 Combustible Gas Control in Containment | |||
WATTS BAR WBNP-112 system is capable of being energized and fully operational within 90 minutes. It is required to operate correctly and continuously following a beyond-design-basis accident. | |||
The HMS, due to its igniter type and locations, redundancy, capability of functioning in a post-accident environment, seismic support, main control room actuation, and remote surviellance, performs its intended function in a manner that provides adequate safety margins. The Unit 2 containment structures can survive the effects of credible degraded core accidents when hydrogen hazards are mitigated by HMS. | |||
6.2.5.4 Testing and Inspections The combustible gas control system is subjected to periodic testing and inspection to demonstrate its availability. | |||
The periodic test program for the containment air return system and the HMS are described in the Technical Specifications. | |||
The periodic test program for the HAS is described in the Technical Requirements Manual. | |||
Preoperational tests are described in Chapter 14. | |||
6.2.5.5 Instrumentation Application The instrumentation design details of the air return fans are shown on Figures 9.4-30 and 9.4-33. The logic, controls and instrumentation of this engineered safety feature system are such that a single failure of any component does not result in the loss of functional capability for the system. | |||
The HAS instrument range is configured to measure from 0-10% hydrogen by volume. | |||
There are two configurable hydrogen concentration alarms, one on the remote control center and one in the main control room. The HAS also provides a trouble alarm to indicate failures of the sensor and pump. An equipment status display monitors pump pressure and flow. | |||
Annunciation is provided in the main control room upon loss of power or undervoltage to the igniters. Each of the two HMS groups is placed in service from the main control room by a handswitch. The igniters are manually energized following any accident which indicates inadequate core cooling. This is done without waiting for a potential hydrogen buildup. | |||
Combustible Gas Control in Containment 6.2.5-5 | |||
WATTS BAR WBNP-112 THIS PAGE INTENTIONALLY BLANK 6.2.5-6 Combustible Gas Control in Containment | |||
WATTS BAR WBNP-112 Figure 6.2.5-1 Deleted by Amendment 95 Combustible Gas Control in Containment 6.2.5-7 | |||
WATTS BAR WBNP-112 Figure 6.2.5-2 Deleted By Amendment 62 6.2.5-8 Combustible Gas Control in Containment | |||
WATTS BAR Combustible Gas Control in Containment Figure 6.2.5-3 Powerhouse Reactor Building Units 1 & 2 - Mechanical Heating, Ventilating and Air Conditioning WBNP-112 6.2.5-9 | |||
6.2.5-10 WATTS BAR Figure 6.2.5-4 Powerhouse Reactor Building Units 1 & 2 - Mechanical Heating, Ventilating and Air Conditioning WBNP-112 Combustible Gas Control in Containment | |||
WATTS BAR Combustible Gas Control in Containment Figure 6.2.5-5 Powerhouse Reactor Building Units 1 & 2 - Mechanical Heating, Ventilation and Air Conditioning WBNP-112 6.2.5-11 | |||
WATTS BAR WBNP-112 Figure 6.2.5-6 Sample Loop Flow Diagram 6.2.5-12 Combustible Gas Control in Containment | |||
WATTS BAR WBNP-112 Figure 6.2.5-7 Deleted by Amendment 95 Combustible Gas Control in Containment 6.2.5-13 | |||
WATTS BAR WBNP-112 Figure 6.2.5-7a Deleted by Amendment 95 6.2.5-14 Combustible Gas Control in Containment | |||
WATTS BAR WBNP-112 Figure 6.2.5-8 Igniter Locations - Lower Compartment and Dead Ended Compartments Combustible Gas Control in Containment 6.2.5-15 | |||
WATTS BAR WBNP-112 Figure 6.2.5-9 Igniter Locations - Lower Compartments 6.2.5-16 Combustible Gas Control in Containment | |||
WATTS BAR WBNP-112 Figure 6.2.5-10 Igniter Locations - Upper Plenum and Upper Compartments Combustible Gas Control in Containment 6.2.5-17 | |||
WATTS BAR WBNP-112 Figure 6.2.5-11 Igniter Locations - Dome 6.2.5-18 Combustible Gas Control in Containment | |||
WATTS BAR WBNP-112 Figure 6.2.5-12 Igniter Locations - Elevation Combustible Gas Control in Containment 6.2.5-19 | |||
WATTS BAR WBNP-112 THIS PAGE INTENTIONALLY BLANK 6.2.5-20 Combustible Gas Control in Containment | |||
WATTS BAR WBNP-112 6.2.6 Containment Leakage Testing Primary containment leakage tests and containment isolation system valve operability tests will be performed periodically to verify that leakage from the containment is maintained within acceptable limits set forth in the Technical Specifications. The types of leakage tests are as follows: | |||
( | (1) Test Type A Tests to measure the reactor primary containment overall integrated leakage rate. The containment leak rate test will be conducted in accordance with 10 CFR 50, Appendix J, Option B. | ||
(2) Test Type B Tests to detect and measure local leaks of containment penetrations, hatches, and personnel locks as required by 10 CFR 50, Appendix J, Option B. | |||
(3) Test Type C Test to detect and measure containment isolation valve leakage as described by 10 CFR 50, Appendix J, Option B. | |||
( | The leakage rate testing pressure for the above tests, Pa (as defined in 10CFR50 Appendix J), has a nominal value of 15.0 psig with allowance for instrument error. | ||
Exceptions to this test pressure are noted elsewhere in this section. | |||
( | 6.2.6.1 Containment Integrated Leak Rate Test The maximum allowable containment leakage rate for the Watts Bar Nuclear Plant is 0.25 weight percent per day as specified in the Technical Specifications. The preoperational testing will be conducted in full compliance with 10 CFR 50, Appendix J as shown in Table 14.2-1. Subsequent periodic testing will also be performed in accordance with Appendix J, Option B with approved exemptions. | ||
Prior to conducting the integrated leak rate test, those lines which penetrate primary containment are aligned as shown in Table 6.2.6-4. | |||
( | The containment is then pressurized in accordance with 10 CFR 50, Appendix J, and the Technical Specification requirements. When test pressure is reached, the containment is isolated from its pressure source and the following parameters are recorded at periodic intervals: | ||
(1) Containment absolute pressure (2) Dry bulb temperatures (3) Water vapor pressures Containment Leakage Testing 6.2.6-1 | |||
( | |||
( | |||
( | |||
WATTS BAR WBNP-112 (4) Outside containment pressure and temperature conditions During the test, ventilation inside the containment is operated as necessary to enhance an even air temperature distribution. The test data are processed at periodic intervals during the test to determine test status and leakage conditions. If it appears that the leakage is excessive, the pressure plateau is either maintained on the test or aborted to perform repairs. The test is run for a prescribed time period to obtain assurance of the test leak rate. | |||
Following the leak rate test, a second leak rate is performed to verify the information obtained in the first test. This verification test consists of slowly bleeding off pressure from containment at a known rate and measuring the total containment leak rate. The superimposed, measured flow is adjusted to a value which causes a change in the weight of air in the containment that is in the same order of magnitude as the allowable leakage rate. | |||
The mass point equations are used to determine the integrated leak rate. The mass point equations will be used for preoperational testing as discussed in Table 14.2-1. | |||
6.2.6.2 Containment Penetration Leakage Rate Test Table 6.2.4-1 lists penetrations in the primary containment. The Type B test is performed on all operational electrical equipment and personnel hatch, fuel transfer tube, Incore Instrumentation Thimble Assembly renewal and ice blowing penetrations, and penetration bellows in accordance with 10 CFR 50, Appendix J, Option B. The dual-ply bellows on containment penetration will be tested at Pa by applying the pressure between the plies. Airlock door seals are tested at 6.0 psig per Technical Specification requirements. Experience has shown that pressurizing the space between the seals to greater than 6.5 psig on personnel airlock doors of the design used at Watts Bar will lift the door and induce gross leakage unless strongbacks are used. Since the door seal test is intended to prove integrity of the seals, it is our position that a test conducted at 6.0 psig will conservatively demonstrate that seal integrity is maintained. | |||
Table 6.2.6-1 lists all penetrations subjected to type B testing. Spare electrical penetrations will be subjected to Type B testing as they become operational. Tables 6.2.4-1 through 6.2.4-4 and Figures 8.3-44 and 8.3-45 give details on these penetrations. The test is performed in full compliance with 10 CFR 50, Appendix J, Option B. The acceptance criteria as required by Appendix J,Option B are specified in the Technical Specifications. | |||
Table 6.2.4-1 lists containment isolation valves. Table 6.2.6-2 identifies those valves that are tested during a Type C test. | |||
Isolation valves that are part of closed systems that are in use after a design basis event and valves that are water sealed for at least 30 days after a design basis event are not tested in the Type C test program (References 1, 2, and 3). Table 6.2.6-3 lists the valves exempted from type C leak testing. Bases for exemptions and exceptions from type C leakage rate testing on a penetration by penetration basis are as follows: | |||
6.2.6-2 Containment Leakage Testing | |||
WATTS BAR WBNP-112 (I) Exemptions (1) Feedwater Bypass - X-8A, X-8B, X-8C, X-8D Feedwater - X-12A, X-12B, X-12C, X-12D Main Steam - X-13A, X-13B, X-13C, X-13D Steam Generator Blowdown - X-14A, X-14B, X-14C, X-14D Steam Generator Blowdown sample line - X-27A, X-27B, X-27C, X-27D Auxiliary Feedwater, X-40A, X-40B These penetrations are directly connected to the secondary side of the steam generator. The main steam and feedwater lines of PWR containments are not required to be Type C tested (see definition of Type C test in 10 CFR 50, Appendix J). These lines are assumed not to rupture as a result of an accident (missile protected). Any leakage through these lines would be identified during operation by the leakage detection program. In addition, during a design basis accident, the secondary side of the steam generator is filled with water and would be at a higher pressure than the containment atmosphere thus preventing outleakage from containment. The integrity of the inside piping is also verified during the Type A test. | |||
(2) CVCS Normal Charging Line, X-16 This penetration uses an inboard check valve and a closed loop outside containment (CLOC) as the means of containment isolation. Type C testing for this path is not required due to the seal pressure greater than 1.1 Pa and the 30-day water seal inventory. A positive pressure preventing air outleakage is assured by the pressure applied against FCV-62-90 and FCV-62-91 (both of which receive a safety injection signal to close) by the high head SI pumps. Water testing for piping integrity is performed in accordance with ASME XI. | |||
(3) RHR Hot Leg Injection, X-17 This penetration uses inboard containment isolation valves and a CLOC for containment boundaries. Type C testing for this penetration is not required since a continuous water seal will be provided at a pressure greater than 1.1 Pa and a 30-day water seal is provided. Water testing for piping integrity is performed in accordance with ASME XI. | |||
(4) RHR Pump Discharge, X-20A, X-20B Same as for X-17. | |||
Containment Leakage Testing 6.2.6-3 | |||
WATTS BAR WBNP-112 (5) SIS Pump Discharge to Hot Leg Injection, X-21, X-32 These lines make use of inboard containment isolation valves and a CLOC for containment boundaries. These lines are postulated to be in-service post accident and the high head pumps will maintain a pressure seal greater than 1.1 Pa for greater than 30 days. | |||
(6) Charging Pump Discharge, X-22 This line makes use of inboard containment isolation valves and a CLOC for containment boundaries. Type C testing is not required for the same reasons as X-21 and X-32. Water seal is provided by the high head pumps. | |||
(7) SIS to Low Head SI, X-33 Same as X-21 and X-32 (8) RCP Seal Injection, X-43A, X-43B, X-43C, X-43D These lines made use of an inboard containment isolation valve and a CLOC for containment boundaries. Type C test is not required for the same reason as given for X-16. | |||
(II) Exceptions (1) Sump Suction to RHR, X-19A, X-19B These lines make use of a containment isolation valve located outside of containment and a CLOC for containment isolation boundaries. During a design basis accident, these lines would be submerged under water which would preclude air outleakage. In addition, these valves are exposed to Pa during each Type A test. | |||
(2) Relief Valve Discharge, X-24 The line uses an inboard containment isolation valve and a CLOC for containment boundaries. The maximum calculated containment accident pressure per 10 CFR 50 Appendix J (Pa) during the design basis accident would not create a substantial outleakage driving force and, in any case, tends to cause the relief valves to seat rather than lift. The systems feeding this line are ECCS and, due either to operating pressure or static head, outleakage would be prevented. Therefore, no Type C testing will be performed for this line. However, this line is exposed to the Pa test pressure during the Type A test. | |||
(3) Containment Spray, X-48A, X-48B and RHR Spray, X-49A, X-49B These lines make use of an inboard containment isolation check valve and a CLOC for containment boundaries of each line. Additionally, a water leg seal exists against a system valve outside containment in each line. This seal 6.2.6-4 Containment Leakage Testing | |||
WATTS BAR WBNP-112 prevents the outleakage of containment atmosphere. An inventory test is performed to ensure a 30-day seal water inventory at a pressure greater than 1.1 Pa, should one spray system shut down. The seal water inventory leakage rate test is performed in lieu of a Type C air leakage rate test of the containment isolation check valves. | |||
(4) RHR Supply to Pumps, X-107 This line makes use of inboard containment isolation valves and a CLOC for containment boundaries. This penetration satisfies ANSI-N271-1976. In addition, an ASME Section XI water leakage test is performed to verify system integrity. Thus, no Type C test is required for this line. | |||
Test connections and pressurizing means are provided to test isolation valves or barriers for leaktightness. Either air or nitrogen is used as the pressurizing medium, depending on the physical location and service of each line. Leak testing of individual valves and penetrations is accomplished by one of the following methods: | |||
(1) Method 1, Pressure Decay The test volume initially shall be pressurized with air or nitrogen to a test pressure greater than the pressure under accident conditions, Pa. The final test pressure shall be greater than Pa. The pressure and temperature shall be recorded at the start and end of the test. The leakage rate shall be calculated from the following formula: | |||
TV P 1 P 2 T stp L i = -------- ------ - ------ ----------- | |||
t T 1 T 2 P stp Where: | |||
Li = Local leak rate, cfm TV = Test volume, ft3 P1 = Initial pressure, psia P2 = Final pressure, psia T1 = Initial temperature, °R T2 = Final temperature, °R Tstp = Standard atmospheric temperature, °R Pstp = Standard atmospheric pressure, psia Containment Leakage Testing 6.2.6-5 | |||
WATTS BAR WBNP-112 t = Test duration, min. | |||
(2) Method 2, - Makeup Flow Rate The test volume shall be pressured and maintained to at least 15 psig using a pressure regulator to maintain test pressure. Makeup fluid flow to the test volume required to maintain test pressure shall be used as the leakage rate of the barrier under test. | |||
The acceptance criteria for the Type C test are given in the Technical Specification which complies with Appendix J to 10 CFR 50, Option B. | |||
6.2.6.3 Scheduling and Reporting of Periodic Tests Type A integrated containment leakage tests are performed prior to operation of the plant and subsequently in accordance with the Containment Leakage Rate Testing Program Type B and Type C leakage rate tests are performed in accordance with the Containment Leakage Rate Testing Program. | |||
Test reports are made in accordance with 10 CFR 50 Appendix J, Option B. | |||
References (1) Title 10, Code of Federal Regulations, Part 50, Appendix J, Option B, Primary Reactor Containment Leakage Testing for Water-Cooled Power Reactors - Performance-Based Requirements. | |||
(2) Regulatory Guide 1.163, Performance-Based Containment Leak-Test Program, September 1995. | |||
(3) NEI 94-01, Revision 0, Industry Guideline for Implementing Performance-Based Option of 10CFR Part 50, Appendix J. | |||
6.2.6-6 Containment Leakage Testing | |||
WATTS BAR WBNP-112 Table 6.2.6-1 Penetrations Subjected To Type B Testing (Page 1 of 3) | |||
Penetration Description X-121E RCP No. 1 - Non-Div. | |||
X-122E RCP No. 2 - Non-Div. | |||
X-123E RCP No. 3 - Non-Div. | |||
X-124E RCP No. 4 - Non-Div. | |||
X-125E 480V Power - Non-Div. | |||
X-126E 480V Power A X-127E 480V Power B X-128E 480V Power A X-129E 480V Power B X-130E Control - Non-Div. | |||
X-131E 480V Power - Non-Div. | |||
X-132E Control Rod Drive Power X-133E Control Rod Drive Power X-134E 480V Power A X-135E 480V Power A X-136E 480V Power B X-137E 480V Power B X-138E Low Level - Non-Div. | |||
X-139E Process Instr. Protection X-140E Incore Instrumentation X-141E 480V Power A X-142E Incore Instrumentation X-143E NIS Channel III X-144E 480V Power - Non-Div. | |||
X-145E Control Rod Pos. Detection X-146E Control Rod Drive Power X-147E Control A X-148E Process Inst. Control X-149E Low Level - Non-Div. | |||
X-150E Annunciation and Communication X-151E NIS Channel IV X-152E 480V Power - Non-Div. | |||
X-153E Low Level - Non-Div. | |||
X-154E Process Inst. Control X-155E 480V Power - Non-Div. | |||
X-156E Control B X-157E Annunciation X-158E Process Inst. Protection X-159E Process Inst. Control Containment Leakage Testing 6.2.6-7 | |||
WATTS BAR WBNP-112 Table 6.2.6-1 Penetrations Subjected To Type B Testing (Page 2 of 3) | |||
Penetration Description X-160E Annunciation and Communication X-161E 480V Power - Non-Div. | |||
X-163E NIS Channel I X-164E Control A X-165E Process Inst. Protection X-166E Control - Non-Div. | |||
X-167E 480V Power - Non-Div. | |||
X-168E Control - Non-Div. | |||
X-169E Process Inst. Protection X-170E Process Inst. Control X-171E Control - Non-Div. | |||
X-172E Control B X-173E Control - Non-Div. | |||
X-174E NIS Channel II X-1 * (Resilient Seal) | |||
X-2A * (Resilient Seal) | |||
X-2B * (Resilient Seal) | |||
X-3 * (Resilient Seal) | |||
X-54 * (Resilient Seal) | |||
X-79A * (Resilient Seal) | |||
X-13A * (Bellows) | |||
X-13B * (Bellows) | |||
X-13C * (Bellows) | |||
X-13D * (Bellows) | |||
X-12A * (Bellows) | |||
X-12B * (Bellows) | |||
X-12C * (Bellows) | |||
X-12D * (Bellows) | |||
X-17 * (Bellows) | |||
X-107 * (Bellows) | |||
X-14A * (Bellows) | |||
X-14B * (Bellows) | |||
X-14C * (Bellows) | |||
X-14D * (Bellows) | |||
X-15 * (Bellows) | |||
X-20A * (Bellows) | |||
X-20B * (Bellows) | |||
X-21 * (Bellows) | |||
X-22 * (Bellows) | |||
X-24 * (Bellows) | |||
X-40D * (Resilient Seal) | |||
X-79B * (Resilient Seal) | |||
X-8A * (Bellows) | |||
X-8B * (Bellows) | |||
X-8C * (Bellows) | |||
X-8D * (Bellows) | |||
X-30 * (Bellows) | |||
X-32 * (Bellows) | |||
X-33 * (Bellows) 6.2.6-8 Containment Leakage Testing | |||
WATTS BAR WBNP-112 Table 6.2.6-1 Penetrations Subjected To Type B Testing (Page 3 of 3) | |||
Penetration Description X-45 * (Bellows) | |||
X-46 * (Bellows) | |||
X-47A * (Bellows) | |||
X-47B * (Bellows) | |||
X-81 * (Bellows) | |||
X-108 * (Resilient Seal) | |||
X-108 * (Bellows) | |||
X-109 * (Resilient Seal) | |||
X-109 * (Bellows) | |||
X-36 * (Resilient Seal) | |||
X-37 * (Resilient Seal) | |||
X-117 * (Resilient Seal) | |||
X-118 * (Resilient Seal) | |||
* See Table 6.2.4-1 for Description. | |||
Containment Leakage Testing 6.2.6-9 | |||
WATTS BAR WBNP-112 Table 6.2.6-2 Containment Isolation Valves Subjected to Type C Testing (Page 1 of 6) | |||
Penetration No. Isolation Valve No. Description X-4 30-56(1) (2) 30-57 30-555 X-5 30-58(1) (2) 30-59 30-554 X-6 30-50(1) (2) 30-51 30-558 X-7 30-52(1) (2) 30-53 30-557 X-9A 30-7 (2) 30-8(1) 30-563 X-9B 30-9 (2) 30-10(1) 30-562 X-10A 30-14 (2) 30-15(1) 30-561 X-10B 30-16 (2) 30-17(1) 30-560 (2) | |||
X-11 30-19 30-20(1) 30-559 (2) | |||
X-15 62-72 62-73 62-74 62-76 62-77 62-662(1) | |||
X-25A 43-11 (2) 43-12 X-25D 43-2 (2) 43-3 6.2.6-10 Containment Leakage Testing | |||
WATTS BAR WBNP-112 Table 6.2.6-2 Containment Isolation Valves Subjected to Type C Testing (Page 2 of 6) | |||
Penetration No. Isolation Valve No. Description (2) | |||
X-26B 52-500 52-504 (2) | |||
X-26A 52-501 52-505 (2) | |||
X-29 70-89 70-92 70-698 (2) | |||
X-30 63-71 63-84 63-23 63-28 (2) | |||
X-31 26-243 26-1296 (2) | |||
X-34 32-111 32-338 32-343 (2) | |||
X-35 70-85 70-703(1) | |||
(2) | |||
X-39A 63-64 63-868 (2) | |||
X-39B 68-305 68-849 (2) | |||
X-41 77-127 77-128 77-2875 (2) | |||
X-42 81-12 81-502 (2) | |||
X-44 62-61 62-63 62-639 (2) | |||
X-45 77-18 77-19 77-20 (2) | |||
X-46 77-9 77-10 84-530 (2) | |||
X-47A 61-191 61-192 61-533 Containment Leakage Testing 6.2.6-11 | |||
WATTS BAR WBNP-112 Table 6.2.6-2 Containment Isolation Valves Subjected to Type C Testing (Page 3 of 6) | |||
Penetration No. Isolation Valve No. Description (2) | |||
X-47B 61-193 61-194 61-680 (2) | |||
X-50A 70-87 70-90 70-687 (2) | |||
X-50B 70-679 70-134 (2) | |||
X-52 70-140 70-100 70-790 (2) | |||
X-53 70-143 (2) | |||
X-56A 67-107 67-113 67-1054D (2) | |||
X-57A 67-111 67-112 67-575D (2) | |||
X-58A 67-83 67-89 67-1054A (2) | |||
X-59A 67-87 67-88 67-575A (2) | |||
X-60A 67-99 67-105 67-1054B (2) | |||
X-61A 67-103 67-104 67-575B (2) | |||
X-62A 67-91 67-97 67-1054C (2) | |||
X-63A 67-95 67-96 67-575C (2) | |||
X-64 31-305 31-306 31-3421 6.2.6-12 Containment Leakage Testing | |||
WATTS BAR WBNP-112 Table 6.2.6-2 Containment Isolation Valves Subjected to Type C Testing (Page 4 of 6) | |||
Penetration No. Isolation Valve No. Description (2) | |||
X-65 31-309 31-308 31-3407 (2) | |||
X-66 31-326 31-327 31-3392 (2) | |||
X-67 31-330 31-329 31-3378 (2) | |||
X-68 67-141 67-580D (2) | |||
X-69 67-130 67-580A (2) | |||
X-70 67-139 67-297 67-585B (2) | |||
X-71 67-134 67-296 67-585C (2) | |||
X-72 67-142 67-298 67-585D (2) | |||
X-73 67-131 67-295 67-585A (2) | |||
X-74 67-138 67-580B (2) | |||
X-75 67-133 67-580C (2) | |||
X-76 33-713 (Unit 1) 33-714 (Unit 1) 33-732 (Unit 2) 33-733 (Unit 2) | |||
(2) | |||
X-77 59-522 59-698 (2) | |||
X-78 26-240 26-1260 Containment Leakage Testing 6.2.6-13 | |||
WATTS BAR WBNP-112 Table 6.2.6-2 Containment Isolation Valves Subjected to Type C Testing (Page 5 of 6) | |||
Penetration No. Isolation Valve No. Description (2) | |||
X-80 30-37 30-40 30-556 (2) | |||
X-81 77-16 77-17 (2) | |||
X-82 78-560 78-561 (2) | |||
X-83 78-557 78-558 (2) | |||
X-84A 68-307 68-308 (2) | |||
X-85B 43-22 43-23 (2) | |||
X-90 32-103 32-318 32-323 (2) | |||
X-91 32-81 32-328 32-333 (2) | |||
X-93 43-34 43-35 (2) | |||
X-94B 90-110 90-111 (2) | |||
X-94C 90-107 90-108 90-109 (2) | |||
X-95B 90-116 90-117 (2) | |||
X-95C 90-113 90-114 90-115 (2) | |||
X-96A 52-506 52-502 (2) | |||
X-96B 52-507 52-503 (2) | |||
X-99 43-202 43-434 6.2.6-14 Containment Leakage Testing | |||
See | WATTS BAR WBNP-112 Table 6.2.6-2 Containment Isolation Valves Subjected to Type C Testing (Page 6 of 6) | ||
Penetration No. Isolation Valve No. Description (2) | |||
X-100 43-201 43-433 (2) | |||
X-114 61-110 61-122 61-745 (2) | |||
X-115 61-96 61-97 61-692 Notes: | |||
(1) These isolation valves are leakage rate tested in the reverse direction. This is acceptable since the results are equivalent or more conservative. | |||
(2) See Table 6.2.4-1 for Description. | |||
Containment Leakage Testing 6.2.6-15 | |||
WATTS BAR WBNP-112 Table 6.2.6-3 Valves Exempted From Type C Leak Testing (Page 1 of 6) | |||
Penetration No. Valve No. System Justification X-8A FCV 3-236 Note 12 Note 1 LCV 3-164 Note 1 LCV 3-174 Note 1 LCV 3-164A Note 1 X-8B FCV 3-239 Note 12 Note 1 X-8C FCV 3-242 Note 12 Note 1 X-8D FCV 3-245 Note 12 Note 1 LCV 3-171 Note 1 LCV 3-175 Note 1 LCV 3-171A Note 1 X-12A FCV 3-33 Note 12 Note 1 X-12B FCV 3-47 Note 12 Note 1 X-12C FCV 3-87 Note 12 Note 1 X-12D FCV 3-100 Note 12 Note 1 X-13A FCV 1-4 Note 12 Note 1 FCV 1-147 Note 1 FCV 1-15 Note 1 DRV 1-536 Note 1 PCV 1-5 Note 1 SFV 1-522 Note 1 SFV 1-523 Note 1 SFV 1-524 Note 1 SFV 1-525 Note 1 SFV 1-526 Note 1 X-13B FCV 1-11 Note 12 Note 1 FCV 1-148 Note 1 PCV 1-12 Note 1 DRV 1-534 Note 1 SFV 1-517 Note 1 SFV 1-518 Note 1 SFV 1-519 Note 1 SFV 1-520 Note 1 SFV 1-521 Note 1 6.2.6-16 Containment Leakage Testing | |||
WATTS BAR WBNP-112 Table 6.2.6-3 Valves Exempted From Type C Leak Testing (Page 2 of 6) | |||
Penetration No. Valve No. System Justification X-13C FCV 1-22 Note 12 Note 1 PCV 1-23 Note 1 FCV 1-149 Note 1 DRV 1-532 Note 1 SFV 1-512 Note 1 SFV 1-513 Note 1 SFV 1-514 Note 1 SFV 1-515 Note 1 SFV 1-516 Note 1 X-13D FCV 1-29 Note 12 Note 1 FCV 1-150 Note 1 PCV 1-30 Note 1 DRV 1-538 Note 1 FCV 1-16 Note 1 SFV 1-527 Note 1 SFV 1-528 Note 1 SFV 1-529 Note 1 FCV 1-530 Note 1 SFV 1-531 Note 1 X-14A FCV 1-14 Note 12 Note 1 X-14B FCV 1-32 Note 12 Note 1 X-14C FCV 1-25 Note 12 Note 1 X-14D FCV 1-7 Note 12 Note 1 X-16 62-543* Note 12 Note 3 X-17 63-640* Note 12 Note 2 63-643* Note 2 FCV 63-158 Note 2 X-19A FCV 63-72 Note 12 Note 5 FCV 72-44 Note 5 X-19B FCV 63-73 Note 12 Note 5 FCV 72-45 Note 5 X-20A FCV 63-112 Note 12 Note 2 63-633* Note 2 63-635* Note 2 X-20B FCV 63-111 Note 12 Note 2 63-632* Note 2 63-634* Note 2 X-21 FCV 63-167 Note 12 Note 6 63-547* Note 6 63-549* Note 6 Containment Leakage Testing 6.2.6-17 | |||
WATTS BAR WBNP-112 Table 6.2.6-3 Valves Exempted From Type C Leak Testing (Page 3 of 6) | |||
Penetration No. Valve No. System Justification X-22 FCV 63-174 Note 12 Note 7 63-581* Note 7 X-24 68-559* Note 12 Note 8 X-27A FCV 43-55 Note 12 Note 1 X-27B FCV 43-58 Note 12 Note 1 X-27C FCV 43-61 Note 12 Note 1 X-27D FCV 43-64 Note 12 Note 1 X-32 FCV 63-21 Note 12 Note 6 63-543* Note 6 63-545* Note 6 6.2.6-18 Containment Leakage Testing | |||
WATTS BAR WBNP-112 Table 6.2.6-3 Valves Exempted From Type C Leak Testing (Page 4 of 6) | |||
Penetration No. Valve No. System Justification X-33 FCV 63-121 Note 12 Note 6 63-551 Note 6 63-553 Note 6 63-555 Note 6 63-557 Note 6 X-40A LCV 3-156 Note 12 Note 1 LCV 3-173 Note 1 LCV 3-156A Note 1 X-40B LCV 3-148 Note 12 Note 1 LCV 3-172 Note 1 LCV 3-148A Note 1 X-43A 62-562* Note 12 Note 9 X-43B 62-561* Note 12 Note 9 X-43C 62-563* Note 12 Note 9 X-43D 62-560* Note 12 Note 9 X-48A 72-548* Note 12 Note 10 X-48B 72-549* Note 12 Note 10 X-49A 72-562* Note 12 Note 10 X-49B 72-563* Note 12 Note 10 X-107 FCV 74-2 Note 12 Note 4 FCV 74-8 Note 4 RFV 74-505 Note 4 FCV 63-185 Note 4 | |||
*Check Valve Containment Leakage Testing 6.2.6-19 | |||
WATTS BAR WBNP-112 Table 6.2.6-3 Valves Exempted From Type C Leak Testing (Page 5 of 6) | |||
Note 1. This penetration is directly connected to the secondary side of the steam generator. | |||
The main steam, feedwater, and steam generator blowdown lines of PWR containments are not required to be tested (see definition of Type C test in 10 CFR 50, Appendix J). | |||
These lines are assumed not to rupture as a result of an accident (missile Protected). | |||
Any leakage through these lines would be identified during operation by the leakage detection program. In addition, during a design basis accident, the secondary side would be at a higher pressure than the containment atmosphere, thus preventing outleakage from containment. The integrity of the inside piping is also verified during the Type A test. | |||
Note 2. This penetration uses inboard containment isolation valves and a CLOC for containment boundaries. Type C testing for this penetration is not required since a continuous water seal will be provided at a pressure greater than 1.1 Pa and a guaranteed 30-day water inventory. Testing will be performed in accordance with ASME XI. | |||
Note 3. This penetration uses an inboard check valve and a closed loop outside containment (CLOC) as the means of containment isolation. Type C testing for this path is not required due to the presence of a 1.1 Pa pressure and a 30-day inventory criteria. A positive pressure preventing air outleakage is assured by the pressure applied against FCV-62-90 and FCV-62-91 (both of which receive a phase A signal) by the high-head SI pumps. Water testing for piping integrity is performed in accordance with ASME XI. | |||
Note 4. This line makes use of inboard containment isolation valves and a CLOC for containment boundaries. This penetration satisfies ANSI-N271-1976. In addition, an ASME Section XI water leakage test will be performed to verify system integrity. | |||
Note 5. This line makes use of a containment isolation valve located outside of containment and a CLOC for containment isolation boundaries. During a design basis accident, this line would be submerged under water which would preclude air outleakage. In addition, these valves are exposed to Pa during each Type A test. | |||
Note 6. This line makes use of inboard containment isolation valves and a CLOC for containment boundaries. These lines are postulated to be inservice post-accident and when not in use, the pumps maintain a pressure seal greater than 1.1 Pa. | |||
6.2.6-20 Containment Leakage Testing | |||
WATTS BAR WBNP-112 Table 6.2.6-3 Valves Exempted From Type C Leak Testing (Page 6 of 6) | |||
Note 7. This line makes use of inboard containment isolation valves and a CLOC for containment boundaries. Type C testing is not required for the same reasons as X-21 and X-32 as stated in Note 6. Water seal is provided by the high-head pumps. | |||
Note 8. This line uses an inboard containment isolation valve and a CLOC for containment boundaries. Pa during the design basis accident would not create a substantial outleakage driving force and, in any case, tend to cause the relief valves in the CLOC to seat rather than lift. The systems feeding this line are ECCS and, due either to operating pressure or static head outleakage would be prevented. This line is exposed to the Pa test pressure during the Type A test. | |||
Note 9. This line makes use of an inboard containment isolation valve and a CLOC for containment boundaries. Type C testing is not required for the same reason as given for X-16 in Note 3. | |||
Note 10. This line makes use of an inboard containment isolation valve and a CLOC for containment boundaries. An inventory test is performed to ensure a 30-day inventory at a pressure greater than 1.1 Pa exists, should one spray system shut down. This will prevent outleakage of containment atmosphere. | |||
Note 11. Not used. | |||
Note 12. See Table 6.2.4-1 for System information. | |||
Containment Leakage Testing 6.2.6-21 | |||
See Note 3 | WATTS BAR WBNP-112 Table 6.2.6-4 Containment Vessel Pressure And Leak Test Reactor Building Containment Penetration Status (Page 1 of 8) | ||
Penetration Description Status A. PENETRATION STATUS DURING TEST PERFORMANCE X-1 (see Note 4.) Closed X-2A (see Note 4.) Closed X-2B (see Note 4.) Closed X-3 (see Note 4.) Closed X-4 (see Note 4.) Vented X-5 (see Note 4.) Vented X-6 (see Note 4.) Vented X-7 (see Note 4.) Vented X-8 (see Note 4.) Vented (see Note 1) | |||
X-8A (see Note 4.) Normal Lineup X-8B (see Note 4.) Normal Lineup X-8C (see Note 4.) Normal Lineup X-8D (see Note 4.) Normal Lineup X-9A (see Note 4.) Vented X-9B (see Note 4.) Vented X-10A (see Note 4.) Vented X-10B (see Note 4.) Vented X-11 (see Note 4.) Vented X-12A (see Note 4.) Normal Lineup X-12B (see Note 4.) Normal Lineup X-12C (see Note 4.) Normal Lineup X-12D (see Note 4.) Normal Lineup X-13A (see Note 4.) Normal Lineup X-13B (see Note 4.) Normal Lineup X-13C (see Note 4.) Normal Lineup X-13D (see Note 4.) Normal Lineup X-14A (see Note 4.) Normal Lineup X-14B (see Note 4.) Normal Lineup X-14C (see Note 4.) Normal Lineup X-14D (see Note 4.) Normal Lineup X-15 (see Note 4.) See Note 3 X-16 (see Note 4.) Normal Lineup X-17 (see Note 4.) Normal Lineup X-18 (see Note 4.) Vented (see Note 1) | |||
X-19A (see Note 4.) Normal Lineup X-19B (see Note 4.) Normal Lineup X-20A (see Note 4.) Normal Lineup 6.2.6-22 Containment Leakage Testing | |||
See Note 3 | WATTS BAR WBNP-112 Table 6.2.6-4 Containment Vessel Pressure And Leak Test Reactor Building Containment Penetration Status (Page 2 of 8) | ||
Penetration Description Status X-20B (see Note 4.) Normal Lineup X-21 (see Note 4.) Normal Lineup X-22 (see Note 4.) Normal Lineup X-23 (see Note 4.) Vented (See Note 1) | |||
X-24 (see Note 4.) Vented X-25A (see Note 4.) See Note 3 X-25B (see Note 4.) Vented (See Note 1) | |||
X-25C (see Note 4.) Vented (See Note 1) | |||
X-25D (see Note 4.) See Note 3 X-26A (see Note 4.) In Use (see Note 2) | |||
X-26B (see Note 4.) In Use (see Note 2) | |||
X-26C (see Note 4.) Normal Lineup X-27A (see Note 4.) Normal Lineup X-27B (see Note 4.) Normal Lineup X-27C (see Note 4.) Normal Lineup X-27D (see Note 4.) Normal Lineup X-28 (see Note 4.) Vented (See Note 1) | |||
X-29 (see Note 4.) See Note 3 X-30 (see Note 4.) See Note 3 X-31 (see Note 4.) See Note 3 X-32 (see Note 4.) Normal Lineup X-33 (see Note 4.) Normal Lineup X-34 (see Note 4.) Vented X-35 (see Note 4.) See Note 3 X-36 (see Note 4.) Vented (see Note 1) | |||
X-37 (see Note 4.) Vented (see Note 1) | |||
X-38 (see Note 4.) Vented (see Note 1) | |||
X-39A (see Note 4.) Vented X-39B (see Note 4.) Vented X-39C (see Note 4.) Vented (see Note 1) | |||
X-39D (see Note 4.) Vented (see Note 1) | |||
X-40A (see Note 4.) Normal Lineup X-40B (see Note 4.) Normal Lineup X-40C (see Note 4.) Vented (see Note 1) | |||
X-40D (see Note 4.) Vented X-41 (see Note 4.) See Note 3 X-42 (see Note 4.) See Note 3 X-43A (see Note 4.) Normal Lineup X-43B (see Note 4.) Normal Lineup X-43C (see Note 4.) Normal Lineup X-43D (see Note 4.) Normal Lineup X-44 (see Note 4.) See Note 3 X-45 (see Note 4.) Vented X-46 (see Note 4.) See Note 3 Containment Leakage Testing 6.2.6-23 | |||
See Note 3 | WATTS BAR WBNP-112 Table 6.2.6-4 Containment Vessel Pressure And Leak Test Reactor Building Containment Penetration Status (Page 3 of 8) | ||
Penetration Description Status X-47A (see Note 4.) In Use X-47B (see Note 4.) In Use X-48A (see Note 4.) Normal Lineup X-48B (see Note 4.) Normal Lineup X-49A (see Note 4.) Normal Lineup X-49B (see Note 4.) Normal Lineup X-50A (see Note 4.) See Note 3 X-50B (see Note 4.) See Note 3 X-51 (see Note 4.) Vented (see Note 1) | |||
X-52 (see Note 4.) See Note 3 X-53 (see Note 4.) See Note 3 X-54 (see Note 4.) In Use X-55 (see Note 4.) Vented (see Note 1) | |||
X-56A (see Note 4.) See Note 3 X-56B (see Note 4.) Vented (see Note 1) | |||
X-57A (see Note 4.) See Note 3 X-57B (see Note 4.) Normal Lineup X-58A (see Note 4.) See Note 3 X-58B (see Note 4.) Normal Lineup X-59A (see Note 4.) See Note 3 X-59B (see Note 4.) Vented (see Note 1) | |||
X-60A (see Note 4.) See Note 3 X-60B (see Note 4.) Normal Lineup X-61A (see Note 4.) See Note 3 X-61B (see Note 4.) Vented (see Note 1) | |||
X-62A (see Note 4.) See Note 3 X-62B (see Note 4.) Vented (see Note 1) | |||
X-63A (see Note 4.) See Note 3 X-63B (see Note 4.) Vented (see Note 1) | |||
X-64 (see Note 4.) See Note 3 X-65 (see Note 4.) See Note 3 X-66 (see Note 4.) See Note 3 X-67 (see Note 4.) See Note 3 X-68 (see Note 4.) See Note 3 X-69 (see Note 4.) See Note 3 X-70 (see Note 4.) See Note 3 X-71 (see Note 4.) See Note 3 X-72 (see Note 4.) See Note 3 X-73 (see Note 4.) See Note 3 X-74 (see Note 4.) See Note 3 X-75 (see Note 4.) See Note 3 X-76 (see Note 4.) Vented X-77 (see Note 4.) See Note 3 6.2.6-24 Containment Leakage Testing | |||
WATTS BAR WBNP-112 Table 6.2.6-4 Containment Vessel Pressure And Leak Test Reactor Building Containment Penetration Status (Page 4 of 8) | |||
(see Note 4.) | Penetration Description Status X-78 (see Note 4.) See Note 3 X-79A (see Note 4.) Vented X-79B (see Note 4.) Vented X-80 (see Note 4.) Vented X-81 (see Note 4.) See Note 3 X-82 (see Note 4.) See Note 3 X-83 (see Note 4.) See Note 3 X-84A (see Note 4.) See Note 3 X-84B (see Note 4.) Normal Lineup X-84C (see Note 4.) Normal Lineup X-84D (see Note 4.) Normal Lineup X-85A (see Note 4.) Vented (see Note 1) | ||
(see Note | X-85B (see Note 4.) See Note 3 X-85C (see Note 4.) Vented (see Note 1) | ||
(see Note 4.) | X-85D (see Note 4.) Vented (see Note 1) | ||
(see Note | X-86A (see Note 4.) Vented (see Note 1) | ||
(see Note 4.) | X-86B (see Note 4.) Vented (see Note 1) | ||
(see Note | X-86C (see Note 4.) Vented (see Note 1) | ||
(see Note 4.) | X-86D (see Note 4.) Vented (see Note 1) | ||
(see Note 4.) | X-87A (see Note 4.) Vented (see Note 1) | ||
(see Note 4.) | X-87B (see Note 4.) Normal Lineup X-87C (see Note 4.) Normal Lineup X-87D (see Note 4.) Normal Lineup X-88 (see Note 4.) Vented (see Note 1) | ||
(see Note 4.) | X-89 (see Note 4.) Vented (see Note 1) | ||
(see Note | X-90 (see Note 4.) Vented X-91 (see Note 4.) Vented X-92A (see Note 4.) Vented (see Note 1) | ||
(see Note 4.) | X-92B (see Note 4.) Vented (see Note 1) | ||
(see Note | X-92C (see Note 4.) Vented (see Note 1) | ||
(see Note 4.) | X-92D (see Note 4.) Vented (see Note 1) | ||
(see Note 4.) | X-93 (see Note 4.) See Note 3 X-94A (see Note 4.) Vented (see Note 1) | ||
(see Note 4.) | X-94B (see Note 4.) Vented X-94C (see Note 4.) Vented X-95A (see Note 4.) Vented (see Note 1) | ||
(see Note | X-95B (see Note 4.) Vented X-95C (see Note 4.) Vented X-96A (see Note 4.) In Use (see Note 2) | ||
(see Note 4.) | X-96B (see Note 4.) In Use (see Note 2) | ||
(see Note | X-96C (see Note 4.) Vented (see Note 1) | ||
(see Note 4.) | X-97 (see Note 4.) Vented (see Note 1) | ||
(see Note | X-98 (see Note 4.) Vented (see Note 1) | ||
(see Note 4.) | Containment Leakage Testing 6.2.6-25 | ||
(see Note | |||
(see Note 4.) | |||
(see Note 4.) | |||
(see Note | |||
(see Note 4.) | |||
(see Note 4.) | |||
(see Note 4.) | |||
(see Note | |||
(see Note 4.) | |||
(see Note 4.) | |||
(see Note 4.) | |||
(see Note | |||
(see Note 4.) | |||
(see Note | |||
(see Note 4.) | |||
(see Note | |||
(see Note 4.) | |||
(see Note | |||
(see Note 4.) | |||
WATTS BAR WBNP-112 Table 6.2.6-4 Containment Vessel Pressure And Leak Test Reactor Building Containment Penetration Status (Page 5 of 8) | |||
Penetration Description Status X-99 (see Note 4.) Vented X-100 (see Note 4.) Vented X-101 (see Note 4.) Vented (see Note 1) | |||
X-102 (see Note 4.) Normal Lineup X-103 (see Note 4.) Vented (see Note 1) | |||
X-104 (see Note 4.) Vented (see Note 1) | |||
X-105 (see Note 4.) Vented (see Note 1) | |||
X-106 (see Note 4.) Vented (see Note 1) | |||
X-107 (see Note 4.) Normal Lineup X-108 (see Note 4.) Vented (see Note 1) | |||
X-109 (see Note 4.) Vented (see Note 1) | |||
X-110 (see Note 4.) Vented (see Note 1) | |||
X-111 (see Note 4.) Vented (see Note 1) | |||
X-112 (see Note 4.) Vented (see Note 1) | |||
X-113 (see Note 4.) Vented (see Note 1) | |||
X-114 (see Note 4.) In Use X-115 (see Note 4.) In Use X-116 (see Note 4.) Vented (see Note 1) | |||
X-117 (see Note 4.) Vented (see Note 1) | |||
X-118 (see Note 4.) In Use X-119 (see Note 4.) Vented (see Note 1) | |||
X-120 (see Note 4.) Vented (see Note 1) | |||
X-121E Electrical Penetration Vented (see Note 1) | |||
X-122E Electrical Penetration Vented (see Note 1) | |||
X-123E Electrical Penetration Vented (see Note 1) | |||
X-124E Electrical Penetration Vented (see Note 1) | |||
X-125E Electrical Penetration Vented (see Note 1) | |||
X-126E Electrical Penetration Vented (see Note 1) | |||
X-127E Electrical Penetration Vented (see Note 1) | |||
X-128E Electrical Penetration Vented (see Note 1) | |||
X-129E Electrical Penetration Vented (see Note 1) | |||
X-130E Electrical Penetration Vented (see Note 1) | |||
X-131E Electrical Penetration Vented (see Note 1) | |||
X-132E Electrical Penetration Vented (see Note 1) | |||
X-133E Electrical Penetration Vented (see Note 1) | |||
X-134E Electrical Penetration Vented (see Note 1) | |||
X-135E Electrical Penetration Vented (see Note 1) | |||
X-136E Electrical Penetration Vented (see Note 1) | |||
X-137E Electrical Penetration Vented (see Note 1) | |||
X-138E Electrical Penetration Vented (see Note 1) | |||
X-139E Electrical Penetration Vented (see Note 1) | |||
X-140E Electrical Penetration Vented (see Note 1) | |||
X-141E Electrical Penetration Vented (see Note 1) | |||
X-142E Electrical Penetration Vented (see Note 1) 6.2.6-26 Containment Leakage Testing | |||
WATTS BAR WBNP-112 Table 6.2.6-4 Containment Vessel Pressure And Leak Test Reactor Building Containment Penetration Status (Page 6 of 8) | |||
Penetration Description Status X-143E Electrical Penetration Vented (see Note 1) | |||
X-144E Electrical Penetration Vented (see Note 1) | |||
X-145E Electrical Penetration Vented (see Note 1) | |||
X-146E Electrical Penetration Vented (see Note 1) | |||
X-147E Electrical Penetration Vented (see Note 1) | |||
X-148E Electrical Penetration Vented (see Note 1) | |||
X-149E Electrical Penetration Vented (see Note 1) | |||
X-150E Electrical Penetration Vented (see Note 1) | |||
X-151E Electrical Penetration Vented (see Note 1) | |||
X-152E Electrical Penetration Vented (see Note 1) | |||
X-153E Electrical Penetration Vented (see Note 1) | |||
X-154E Electrical Penetration Vented (see Note 1) | |||
X-155E Electrical Penetration Vented (see Note 1) | |||
X-156E Electrical Penetration Vented (see Note 1) | |||
X-157E Electrical Penetration Vented (see Note 1) | |||
X-158E Electrical Penetration Vented (see Note 1) | |||
X-159E Electrical Penetration Vented (see Note 1) | |||
X-160E Electrical Penetration Vented (see Note 1) | |||
X-161E Electrical Penetration Vented (see Note 1) | |||
X-162E Seal Welded Spare Vented (see Note 1) | |||
X-163E Electrical Penetration Vented (see Note 1) | |||
X-164E Electrical Penetration Vented (see Note 1) | |||
X-165E Electrical Penetration Vented (see Note 1) | |||
X-166E Electrical Penetration Vented (see Note 1) | |||
X-167E Electrical Penetration Vented (see Note 1) | |||
X-168E Electrical Penetration Vented (see Note 1) | |||
X-169E Electrical Penetration Vented (see Note 1) | |||
X-170E Electrical Penetration Vented (see Note 1) | |||
X-171E Electrical Penetration Vented (see Note 1) | |||
X-172E Electrical Penetration Vented (see Note 1) | |||
X-173E Electrical Penetration Vented (see Note 1) | |||
X-174E Electrical Penetration Vented (see Note 1) | |||
Containment Leakage Testing 6.2.6-27 | |||
WATTS BAR WBNP-112 Table 6.2.6-4 Containment Vessel Pressure And Leak Test Reactor Building Containment Penetration Status (Page 7 of 8) | |||
Penetration Description Status B. TESTABLE PENETRATIONS REQUIRED TO BE INSERVICE DURING TEST PERFORMANCE X-20A (see Note 4) Residual heat removal system required X-20B (see Note 4) inservice to remove decay heat from fuel X-26A (see Note 4) Isolation valves required to be open to X-26B monitor containment pressure (see Note 2) | |||
X-47A (see Note 4) Glycol cooling supply to air handling units in ice condenser required to ensure ice condition is maintained X-47B (see Note 4) Glycol cooling return from air handling units in ice condenser required to ensure ice condition is maintained X-54 (see Note 4) Used as pressurization point for air compressors X-96A (see Note 4) Isolation valves required to be open to X-96B monitor containment pressure (see Note 2) | |||
X-107 (see Note 4) Residual heat removal system required inservice to remove decay heat from fuel X-114 (see Note 4) Glycol return line from floor cooling coils required to ensure ice condition is maintained X-115 (see Note 4) Glycol supply line to floor cooling coils required to ensure ice condition is maintained 6.2.6-28 Containment Leakage Testing | |||
WATTS BAR WBNP-112 Table 6.2.6-4 Containment Vessel Pressure And Leak Test Reactor Building Containment Penetration Status (Page 8 of 8) | |||
Penetration Description Status X-118 (See Note 4) Used as source for verification flow and post-test depressurization; opened during DBF event to drain water from annulus to Reactor Building floor and equipment drain sump Notes: | |||
: 1. These penetrations are closed. Venting is provided by the design of the penetration such that any leakage is detectable by the integrated leak rate test. | |||
: 2. These penetrations are designed to facilitate ILRT performance. It may not be necessary to utilize all of the penetrations. If not in use, the penetration is vented. | |||
: 3. These penetrations may remain water filled and/or unvented to facilitate planning and scheduling or for ALARA consideration provided they have been Type B or C tested within the previous 24 months. | |||
: 4. See Table 6.2.4-1 for Description. | |||
Containment Leakage Testing 6.2.6-29 | |||
WATTS BAR WBNP-112 THIS PAGE INTENTIONALLY BLANK 6.2.6-30 Containment Leakage Testing}} | |||
Latest revision as of 20:41, 5 February 2020
| ML14160B106 | |
| Person / Time | |
|---|---|
| Site: | Watts Bar  |
| Issue date: | 05/30/2014 |
| From: | Tennessee Valley Authority |
| To: | Office of Nuclear Reactor Regulation |
| Shared Package | |
| ML14160A901 | List:
|
| References | |
| Download: ML14160B106 (516) | |
Text
WATTS BAR TABLE OF CONTENTS Section Title Page 6.0 ENGINEERED SAFETY FEATURES 6.1 ENGINEERED SAFETY FEATURE MATERIALS 6.1-1 6.1.1 METALLIC MATERIALS 6.1-1 6.1.1.1 MATERIALS SELECTION AND FABRICATION 6.1-1 6.1.1.2 COMPOSITION, COMPATIBILITY, AND STABILITY OF CONTAINMENT AND CORE SPRAY COOLANTS 6.1-2 6.1.2 ORGANIC MATERIALS 6.1-3 6.1.2.1 ELECTRICAL INSULATION 6.1-3 6.1.2.2 SURFACE COATINGS 6.1-3 6.1.2.3 ICE CONDENSER EQUIPMENT 6.1-4 6.1.2.4 IDENTIFICATION TAGS 6.1-4 6.1.2.5 VALVES AND INSTRUMENTS WITHIN CONTAINMENT 6.1-4 6.1.2.6 HEATING AND VENTILATING DOOR SEALS 6.1-5 6.1.2.7 MISCELLANEOUS 6.1-5 6.1.3 POST-ACCIDENT CHEMISTRY 6.1-5 6.1.3.1 BORIC ACID, H3BO3 6.1-5 6.1.3.2 LITHIUM HYDROXIDE 6.1-5 6.1.3.3 SODIUM TETRABORATE 6.1-5 6.1.3.4 FINAL POST-ACCIDENT CHEMISTRY 6.1-6 6.1.4 DEGREE OF COMPLIANCE WITH REGULATORY GUIDE 1.54 FOR PAINTS AND COATINGS INSIDE CONTAINMENT 6.1-6 6.2 CONTAINMENT SYSTEMS 6.2.1 CONTAINMENT FUNCTIONAL DESIGN 6.2.1-1 6.2.1.1 DESIGN BASES 6.2.1-1 6.2.1.1.1 PRIMARY CONTAINMENT DESIGN BASES 6.2.1-1 6.2.1.2 PRIMARY CONTAINMENT SYSTEM DESIGN 6.2.1-3 6.2.1.3 DESIGN EVALUATION 6.2.1-3 6.2.1.3.1 PRIMARY CONTAINMENT EVALUATION 6.2.1-3 6.2.1.3.2 GENERAL DESCRIPTION OF CONTAINMENT PRESSURE ANALYSIS 6.2.1-4 6.2.1.3.3 LONG-TERM CONTAINMENT PRESSURE ANALYSIS 6.2.1-4 6.2.1.3.4 SHORT-TERM BLOWDOWN ANALYSIS 6.2.1-8 Table of Contents 6-i
WATTS BAR TABLE OF CONTENTS Section Title Page 6.2.1.3.5 EFFECT OF STEAM BYPASS 6.2.1-17 6.2.1.3.6 MASS AND ENERGY RELEASE DATA 6.2.1-21 6.2.1.3.7 ACCIDENT CHRONOLOGY 6.2.1-29 6.2.1.3.8 MASS AND ENERGY BALANCE TABLES 6.2.1-29 6.2.1.3.9 CONTAINMENT PRESSURE DIFFERENTIALS 6.2.1-31 6.2.1.3.10 STEAM LINE BREAK INSIDE CONTAINMENT 6.2.1-34 6.2.1.3.11 MAXIMUM REVERSE PRESSURE DIFFERENTIALS 6.2.1-39 6.2.2 CONTAINMENT HEAT REMOVAL SYSTEMS 6.2.2-1 6.2.2.1 DESIGN BASES 6.2.2-1 6.2.2.2 SYSTEM DESIGN 6.2.2-3 6.2.2.3 DESIGN EVALUATION 6.2.2-5 6.2.2.4 TESTING AND INSPECTIONS 6.2.2-7 6.2.2.5 INSTRUMENTATION REQUIREMENTS 6.2.2-8 6.2.2.6 MATERIALS 6.2.2-9 6.2.3 SECONDARY CONTAINMENT FUNCTIONAL DESIGN 6.2.3-1 6.2.3.1 DESIGN BASES 6.2.3-1 6.2.3.1.1 SECONDARY CONTAINMENT ENCLOSURES 6.2.3-1 6.2.3.1.2 EMERGENCY GAS TREATMENT SYSTEM (EGTS) 6.2.3-1 6.2.3.1.3 AUXILIARY BUILDING GAS TREATMENT SYSTEM (ABGTS) 6.2.3-2 6.2.3.2 SYSTEM DESIGN 6.2.3-2 6.2.3.2.1 SECONDARY CONTAINMENT ENCLOSURES 6.2.3-2 6.2.3.2.2 EMERGENCY GAS TREATMENT SYSTEM (EGTS) 6.2.3-6 6.2.3.2.3 AUXILIARY BUILDING GAS TREATMENT SYSTEM (ABGTS) 6.2.3-10 6.2.3.3 DESIGN EVALUATION 6.2.3-12 6.2.3.3.1 SECONDARY CONTAINMENT ENCLOSURES 6.2.3-12 6.2.3.3.2 EMERGENCY GAS TREATMENT SYSTEM (EGTS) 6.2.3-15 6.2.3.3.3 AUXILIARY BUILDING GAS TREATMENT SYSTEM (ABGTS) 6.2.3-19 6.2.3.3.4 TRITIUM PRODUCTION CORE EVALUATION (UNIT 1 ONLY) 6.2.3-22 6.2.3.4 TEST AND INSPECTIONS 6.2.3-22 6.2.3.4.1 EMERGENCY GAS TREATMENT SYSTEM (EGTS) 6.2.3-22 6.2.3.4.2 AUXILIARY BUILDING GAS TREATMENT SYSTEM (ABGTS) 6.2.3-23 6.2.3.5 INSTRUMENTATION REQUIREMENTS 6.2.3-23 6.2.3.5.1 EMERGENCY GAS TREATMENT SYSTEM (EGTS) 6.2.3-23 Table of Contents 6-ii
WATTS BAR TABLE OF CONTENTS Section Title Page 6.2.3.5.2 AUXILIARY BUILDING GAS TREATMENT SYSTEM (ABGTS) 6.2.3-24 6.2.4 CONTAINMENT ISOLATION SYSTEMS 6.2.4-1 6.2.4.1 DESIGN BASES 6.2.4-1 6.2.4.2 SYSTEM DESIGN 6.2.4-4 6.2.4.2.1 DESIGN REQUIREMENTS 6.2.4-5 6.2.4.2.2 CONTAINMENT ISOLATION OPERATION 6.2.4-6 6.2.4.2.3 PENETRATION DESIGN 6.2.4-7 6.2.4.3 DESIGN EVALUATION 6.2.4-12 6.2.4.3.1 POSSIBLE LEAKAGE PATHS 6.2.4-15 6.2.4.4 TESTS AND INSPECTIONS 6.2.4-17 6.2.5 COMBUSTIBLE GAS CONTROL IN CONTAINMENT 6.2.5-1 6.2.5.1 DESIGN BASES 6.2.5-1 6.2.5.2 SYSTEM DESIGN 6.2.5-2 6.2.5.3 DESIGN EVALUATION 6.2.5-4 6.2.5.4 TESTING AND INSPECTIONS 6.2.5-5 6.2.5.5 INSTRUMENTATION APPLICATION 6.2.5-5 6.2.6 CONTAINMENT LEAKAGE TESTING 6.2.6-1 6.2.6.1 CONTAINMENT INTEGRATED LEAK RATE TEST 6.2.6-1 6.2.6.2 CONTAINMENT PENETRATION LEAKAGE RATE TEST 6.2.6-2 6.2.6.3 SCHEDULING AND REPORTING OF PERIODIC TESTS 6.2.6-6 6.3 EMERGENCY CORE COOLING SYSTEM 6.3-1 6.3.1 DESIGN BASES 6.3-1 6.3.1.1 RANGE OF COOLANT RUPTURES AND LEAKS 6.3-1 6.3.1.2 FISSION PRODUCT DECAY HEAT 6.3-2 6.3.1.3 REACTIVITY REQUIRED FOR COLD SHUTDOWN 6.3-2 6.3.1.4 CAPABILITY TO MEET FUNCTIONAL REQUIREMENTS 6.3-2 6.3.2 SYSTEM DESIGN 6.3-2 6.3.2.1 SCHEMATIC PIPING AND INSTRUMENTATION DIAGRAMS 6.3-2 6.3.2.2 EQUIPMENT AND COMPONENT DESIGN 6.3-2 6.3.2.3 APPLICABLE CODES AND CLASSIFICATIONS 6.3-16 6.3.2.4 MATERIALS SPECIFICATIONS AND COMPATIBILITY 6.3-16 6.3.2.5 DESIGN PRESSURES AND TEMPERATURES 6.3-16 Table of Contents 6-iii
WATTS BAR TABLE OF CONTENTS Section Title Page 6.3.2.6 COOLANT QUANTITY 6.3-17 6.3.2.7 PUMP CHARACTERISTICS 6.3-17 6.3.2.8 HEAT EXCHANGER CHARACTERISTICS 6.3-17 6.3.2.9 ECCS FLOW DIAGRAMS 6.3-17 6.3.2.10 RELIEF VALVES 6.3-17 6.3.2.11 SYSTEM RELIABILITY 6.3-17 6.3.2.12 PROTECTION PROVISIONS 6.3-22 6.3.2.13 PROVISIONS FOR PERFORMANCE TESTING 6.3-22 6.3.2.14 NET POSITIVE SUCTION HEAD 6.3-22 6.3.2.15 CONTROL OF MOTOR-OPERATED ISOLATION VALVES 6.3-23 6.3.2.16 MOTOR-OPERATED VALVES AND CONTROLS 6.3-23 6.3.2.17 MANUAL ACTIONS 6.3-23 6.3.2.18 PROCESS INSTRUMENTATION 6.3-23 6.3.2.19 MATERIALS 6.3-24 6.3.3 PERFORMANCE EVALUATION 6.3-24 6.3.3.1 EVALUATION MODEL 6.3-24 6.3.3.2 ECCS PERFORMANCE 6.3-24 6.3.3.3 ALTERNATE ANALYSIS METHODS 6.3-24 6.3.3.4 FUEL ROD PERFORATIONS 6.3-25 6.3.3.5 EFFECTS OF ECCS OPERATION ON THE CORE 6.3-25 6.3.3.6 USE OF DUAL FUNCTION COMPONENTS 6.3-26 6.3.3.7 LAG TIMES 6.3-27 6.3.3.8 THERMAL SHOCK CONSIDERATIONS 6.3-28 6.3.3.9 LIMITS ON SYSTEM PARAMETERS 6.3-28 6.3.3.10 USE OF RHR SPRAY 6.3-28 6.3.4 TESTS AND INSPECTIONS 6.3-29 6.3.4.1 PREOPERATIONAL TESTS 6.3-29 6.3.4.2 COMPONENT TESTING 6.3-29 6.3.4.3 PERIODIC SYSTEM TESTING 6.3-30 6.3.5 INSTRUMENTATION APPLICATION 6.3-30 6.3.5.1 TEMPERATURE INDICATION 6.3-30 6.3.5.2 PRESSURE INDICATION 6.3-30 6.3.5.3 FLOW INDICATION 6.3-31 6.3.5.4 LEVEL INDICATION 6.3-31 Table of Contents 6-iv
WATTS BAR TABLE OF CONTENTS Section Title Page 6.3.5.5 VALVE POSITION INDICATION 6.3-32 6.4 HABITABILITY SYSTEMS 6.4-1 6.4.1 DESIGN BASES 6.4-1 6.4.2 SYSTEM DESIGN 6.4-1 6.4.2.1 DEFINITION OF MCRHS AREA 6.4-1 6.4.2.2 VENTILATION SYSTEM DESIGN 6.4-2 6.4.2.3 LEAK TIGHTNESS 6.4-2 6.4.2.4 INTERACTION WITH OTHER ZONES AND PRESSURE-CONTAINING EQUIPMENT 6.4-3 6.4.2.5 SHIELDING DESIGN 6.4-4 6.4.2.6 CONTROL ROOM EMERGENCY PROVISIONS 6.4-4 6.4.2.7 MCRHS FIRE PROTECTION 6.4-4 6.4.3 SYSTEM OPERATIONAL PROCEDURES 6.4-5 6.4.4 DESIGN EVALUATIONS 6.4-7 6.4.4.1 RADIOLOGICAL PROTECTION 6.4-7 6.4.4.2 TOXIC GAS PROTECTION 6.4-7 6.4.5 TESTING AND INSPECTION 6.4-9 6.4.6 INSTRUMENTATION REQUIREMENTS 6.4-9 6.5 FISSION PRODUCT REMOVAL AND CONTROL SYSTEMS 6.5-1 6.5.1 ENGINEERED SAFETY FEATURE (ESF) FILTER SYSTEMS 6.5-1 6.5.1.1 DESIGN BASES 6.5-1 6.5.1.2 SYSTEM DESIGN 6.5-2 6.5.1.3 DESIGN EVALUATION 6.5-4 6.5.1.4 TESTS AND INSPECTIONS 6.5-5 6.5.1.5 INSTRUMENTATION REQUIREMENTS 6.5-5 6.5.1.6 MATERIALS 6.5-6 6.5.2 CONTAINMENT SPRAY SYSTEM FOR FISSION PRODUCT CLEANUP 6.5-7 6.5.2.1 DESIGN BASES 6.5-7 6.5.2.2 SYSTEM DESIGN 6.5-7 6.5.2.3 DESIGN EVALUATION 6.5-7 6.5.2.4 TESTS AND INSPECTIONS 6.5-7 6.5.2.5 INSTRUMENTATION REQUIREMENTS 6.5-7 6.5.2.6 MATERIALS 6.5-7 Table of Contents 6-v
WATTS BAR TABLE OF CONTENTS Section Title Page 6.5.3 FISSION PRODUCT CONTROL SYSTEMS 6.5-7 6.5.3.1 PRIMARY CONTAINMENT 6.5-7 6.5.3.2 SECONDARY CONTAINMENTS 6.5-9 6.5.4 ICE CONDENSER AS A FISSION PRODUCT CLEANUP SYSTEM 6.5-10 6.5.4.1 ICE CONDENSER DESIGN BASIS (FISSION PRODUCT CLEANUP FUNCTION) 6.5-10 6.5.4.2 ICE CONDENSER SYSTEM DESIGN 6.5-10 6.5.4.3 ICE CONDENSER SYSTEM DESIGN EVALUATION (FISSION PRODUCT CLEANUP FUNCTION) 6.5-11 6.5.4.4 CONDENSER SYSTEM TESTS AND INSPECTIONS 6.5-13 6.5.4.5 ICE CONDENSER MATERIALS 6.5-13 6.6 INSERVICE INSPECTION OF ASME CODE CLASS 2 AND 3 COMPONENTS 6.6-1 6.6.1 COMPONENTS SUBJECT TO EXAMINATION AND/OR TEST 6.6-1 6.6.2 ACCESSIBILITY 6.6-1 6.6.3 EXAMINATION TECHNIQUES AND PROCEDURES 6.6-1 6.6.4 INSPECTION INTERVALS 6.6-1 6.6.5 EXAMINATION CATEGORIES AND REQUIREMENTS 6.6-1 6.6.6 EVALUATION OF EXAMINATION RESULTS 6.6-1 6.6.7 SYSTEM PRESSURE TESTS 6.6-2 6.6.8 PROTECTION AGAINST POSTULATED PIPING FAILURES 6.6-2 6.7 ICE CONDENSER SYSTEM 6.7-1 6.7.1 FLOOR STRUCTURE AND COOLING SYSTEM 6.7-1 6.7.1.1 DESIGN BASES 6.7-1 6.7.1.2 SYSTEM DESIGN 6.7-4 6.7.1.3 DESIGN EVALUATION 6.7-5 6.7.2 WALL PANELS 6.7-8 6.7.2.1 DESIGN BASIS 6.7-8 6.7.2.2 SYSTEM DESIGN 6.7-8 6.7.2.3 DESIGN EVALUATION 6.7-9 6.7.3 LATTICE FRAMES AND SUPPORT COLUMNS 6.7-9 6.7.3.1 DESIGN BASIS 6.7-9 6.7.3.2 SYSTEM DESIGN 6.7-12 6.7.3.3 DESIGN EVALUATION 6.7-13 Table of Contents 6-vi
WATTS BAR TABLE OF CONTENTS Section Title Page 6.7.4 ICE BASKETS 6.7-14 6.7.4.1 DESIGN BASIS 6.7-14 6.7.4.2 SYSTEM DESIGN 6.7-16 6.7.4.3 DESIGN EVALUATION 6.7-18 6.7.5 CRANE AND RAIL ASSEMBLY 6.7-20 6.7.5.1 DESIGN BASIS 6.7-20 6.7.5.2 SYSTEM DESIGN 6.7-21 6.7.5.3 DESIGN EVALUATION 6.7-21 6.7.6 REFRIGERATION SYSTEM 6.7-22 6.7.6.1 DESIGN BASIS 6.7-22 6.7.6.2 SYSTEM DESIGN 6.7-23 6.7.6.3 DESIGN EVALUATION 6.7-26 6.7.7 AIR HANDLING UNITS 6.7-30 6.7.7.1 DESIGN BASIS 6.7-30 6.7.7.2 SYSTEM DESIGN 6.7-31 6.7.7.3 DESIGN EVALUATION 6.7-31 6.7.8 LOWER INLET DOORS 6.7-32 6.7.8.1 DESIGN BASIS 6.7-32 6.7.8.2 SYSTEM DESIGN 6.7-35 6.7.8.3 DESIGN EVALUATION 6.7-37 6.7.9 LOWER SUPPORT STRUCTURE 6.7-38 6.7.9.1 DESIGN BASIS 6.7-38 6.7.9.2 SYSTEM DESIGN 6.7-39 6.7.9.3 DESIGN EVALUATION 6.7-41 6.7.10 TOP DECK AND DOORS 6.7-50 6.7.10.1 DESIGN BASIS 6.7-50 6.7.10.2 SYSTEM DESIGN 6.7-51 6.7.11 INTERMEDIATE DECK AND DOORS 6.7-55 6.7.11.1 DESIGN BASIS 6.7-55 6.7.11.2 SYSTEM DESIGN 6.7-56 6.7.11.3 DESIGN EVALUATION 6.7-57 6.7.12 AIR DISTRIBUTION DUCTS 6.7-58 6.7.12.1 DESIGN BASIS 6.7-58 6.7.12.2 SYSTEM DESIGN 6.7-59 Table of Contents 6-vii
WATTS BAR TABLE OF CONTENTS Section Title Page 6.7.12.3 DESIGN EVALUATION 6.7-59 6.7.13 EQUIPMENT ACCESS DOOR 6.7-59 6.7.13.1 DESIGN BASIS 6.7-59 6.7.13.2 SYSTEM DESIGN 6.7-60 6.7.13.3 DESIGN EVALUATION 6.7-60 6.7.14 ICE TECHNOLOGY, ICE PERFORMANCE, AND ICE CHEMISTRY 6.7-60 6.7.14.1 DESIGN BASIS 6.7-60 6.7.14.2 SYSTEM DESIGN 6.7-61 6.7.14.3 DESIGN EVALUATION 6.7-61 6.7.15 ICE CONDENSER INSTRUMENTATION 6.7-66 6.7.15.1 DESIGN BASIS 6.7-66 6.7.15.2 DESIGN DESCRIPTION 6.7-67 6.7.15.3 DESIGN EVALUATION 6.7-69 6.7.16 ICE CONDENSER STRUCTURAL DESIGN 6.7-69 6.7.16.1 APPLICABLE CODES, STANDARDS, AND SPECIFICATIONS 6.7-69 6.7.16.2 LOADS AND LOADING COMBINATIONS 6.7-69 6.7.16.3 DESIGN AND ANALYTICAL PROCEDURES 6.7-70 6.7.16.4 STRUCTURAL ACCEPTANCE CRITERIA 6.7-71 6.7.17 SEISMIC ANALYSIS 6.7-72 6.7.17.1 SEISMIC ANALYSIS METHODS 6.7-72 6.7.17.2 SEISMIC LOAD DEVELOPMENT 6.7-74 6.7.17.3 VERTICAL SEISMIC RESPONSE 6.7-76 6.7.18 MATERIALS 6.7-76 6.7.18.1 DESIGN CRITERIA 6.7-76 6.7.18.2 ENVIRONMENTAL EFFECTS 6.7-77 6.7.18.3 COMPLIANCE WITH 10 CFR 50, APPENDIX B 6.7-78 6.7.18.4 MATERIALS SPECIFICATIONS 6.7-79 6.7.19 TESTS AND INSPECTIONS 6.7-80 6.8 AIR RETURN FANS 6.8-1 6.8.1 DESIGN BASES 6.8-1 6.8.2 SYSTEM DESCRIPTION 6.8-1 6.8.3 SAFETY EVALUATION 6.8-2 6.8.4 INSPECTION AND TESTING 6.8-3 6.8.5 INSTRUMENTATION REQUIREMENTS 6.8-3 Table of Contents 6-viii
WATTS BAR TABLE OF CONTENTS Section Title Page 6.9 MOTOR-OPERATED VALVE (MOV) PROGRAMS6.9-1 Table of Contents 6-ix
WATTS BAR TABLE OF CONTENTS Section Title Page THIS PAGE INTENTIONALLY BLANK Table of Contents 6-x
WATTS BAR LIST OF TABLES Section Title TABLE 6.1-1 DELETED BY AMENDMENT 97 TABLE 6.2.1-1 STRUCTURAL HEAT SINKS TABLE 6.2.1-2 PUMP FLOW RATES VS. TIME TABLE 6.2.1-3 ENERGY BALANCES TABLE 6.2.1-4 ENERGY BALANCES TABLE 6.2.1-5 MATERIAL PROPERTY DATA TABLE 6.2.1-6 TMD INPUT FOR WATTS BAR TABLE 6.2.1-7 TMD FLOW INPUT DATA FOR WATTS BAR TABLE 6.2.1-8 CALCULATED MAXIMUM PEAK PRESSURES IN LOWER COMPARTMENT ELEMENTS ASSUMING UNAUGMENTED FLOW TABLE 6.2.1-9 CALCULATED MAXIMUM PEAK PRESSURES IN THE ICE CONDENSER COMPARTMENT ASSUMING UNAUGMENTED FLOW TABLE 6.2.1-10 CALCULATED MAXIMUM DIFFERENTIAL PRESSURES ACROSS THE OPERATING DECK OR LOWER CRANE WALL ASSUMING UNAUGMENTED FLOW TABLE 6.2.1-11 CALCULATED MAXIMUM DIFFERENTIAL PRESSURES ACROSS THE UPPER CRANE WALL ASSUMING UNAUGMENTED FLOW TABLE 6.2.1-12 SENSITIVITY STUDIES FOR D. C. COOK PLANT TABLE 6.2.1-13 WATTS BAR ICE CONDENSER DESIGN PARAMETERS TABLE 6.2.1-14 ALLOWABLE LEAKAGE AREA FOR VARIOUS REACTOR COOLANT SYSTEM BREAK SIZES TABLE 6.2.1-15 SYSTEM PARAMETERS INITIAL CONDITIONS TABLE 6.2.1-16 DOUBLE-ENDED PUMP SUCTION GUILLOTINE BREAK -
BLOWDOWN MASS AND ENERGY RELEASES TABLE 6.2.1-17 DOUBLE-ENDED PUMP SUCTION GUILLOTINE BREAK -
REFLOOD MASS AND ENERGY RELEASE - MINIMUM SAFETY INJECTION TABLE 6.2.1-18 DOUBLE-ENDED PUMP SUCTION GUILLOTINE BREAK -
MINIMUM SAFETY INJECTION PRINCIPAL PARAMETERS DURING REFLOOD TABLE 6.2.1-19 DOUBLE-ENDED PUMP SUCTION GUILLOTINE BREAK -
POST-REFLOOD MASS AND ENERGY RELEASES - MINIMUM SAFETY INJECTION TABLE 6.2.1-20 DECAY HEAT CURVE List of Tables 6-xi
WATTS BAR LIST OF TABLES Section Title TABLE 6.2.1-21 DELETED BY AMENDMENT 97 TABLE 6.2.1-22 DELETED BY AMENDMENT 97 TABLE 6.2.1-23 BREAK MASS AND ENERGY FLOW FROM A DOUBLE-ENDED COLD LEG GUILLOTINE BREAK TABLE 6.2.1-24 BREAK MASS AND ENERGY FLOW FROM A DOUBLE-ENDED HOT LEG GUILLOTINE BREAK TABLE 6.2.1-25 DOUBLE-ENDED PUMP SUCTION LOCA SEQUENCE OF EVENTS TABLE 6.2.1-26A DOUBLE-ENDED PUMP SUCTION GUILLOTINE BREAK MINIMUM SAFETY INJECTION - MASS BALANCE TABLE 6.2.1-26B DOUBLE-ENDED PUMP SUCTION GUILLOTINE BREAK MINIMUM SAFETY INJECTION - ENERGY BALANCE TABLE 6.2.1-27A STEAM LINE BREAK BLOWDOWN TABLE 6.2.1-27B STEAM GENERATOR ENCLOSURE GEOMETRY TABLE 6.2.1-27C STEAM GENERATOR ENCLOSURE FLOW PATH DATA TABLE 6.2.1-27D PEAK DIFFERENTIAL PRESSURE - STEAM GENERATOR ENCLOSURE TABLE 6.2.1-28 MASS AND ENERGY RELEASE RATES INTO PRESSURIZER ENCLOSURE TABLE 6.2.1-29A PRESSURIZER GEOMETRIC DATA TABLE 6.2.1-29B PEAK DIFFERENTIAL PRESSURE - PRESSURIZER ENCLOSURE TABLE 6.2.1-30 MASS AND ENERGY RELEASE RATES 127 IN2 COLD LEG TABLE 6.2.1-31 REACTOR CAVITY VOLUMES TABLE 6.2.1-32 FLOW PATH DATA (REACTOR CAVITY)
TABLE 6.2.1-33 CONTAINMENT DATA (ECCS ANALYSIS)
TABLE 6.2.1-34 MAJOR CHARACTERISTICS OF STRUCTURAL HEAT SINKS INSIDE SEQUOYAH NUCLEAR PLANT CONTAINMENT -
UPPER COMPARTMENT TABLE 6.2.1-35 MAJOR CHARACTERISTICS OF STRUCTURAL HEAT SINKS INSIDE SEQUOYAH NUCLEAR PLANT CONTAINMENT -
LOWER COMPARTMENT TABLE 6.2.1-36 MAJOR CHARACTERISTICS OF STRUCTURAL HEAT SINKS INSIDE SEQUOYAH NUCLEAR PLANT CONTAINMENT -
DEAD-ENDED COMPARTMENT TABLE 6.2.1-37 MAXIMUM REVERSE PRESSURE DIFFERENTIAL PRESSURE ANALYSIS BASE CASE List of Tables 6-xii
WATTS BAR LIST OF TABLES Section Title TABLE 6.2.1-38 ICE CONDENSER STEAM EXIT FLOW VS. TIME VS. SUMP TEMPERATURE TABLE 6.2.1-39 MASS AND ENERGY RELEASE RATES FOR SPECIFIED STEAM LINE BREAKS TABLE 6.2.1-39 MASS AND ENERGY RELEASE RATES FOR SPECIFIED STEAM LINE BREAKS (CONTD)
TABLE 6.2.1-39 MASS AND ENERGY RELEASE RATES FOR SPECIFIED STEAM LINE BREAKS (CONTD)
TABLE 6.2.1-40 STEAM LINE BREAK CASES FOR CORE INTEGRITY TABLE 6.2.1-41 LINE BREAK(1) DESCRIPTIONS FOR MASS AND ENERGY RELEASES TABLE 6.2.1-42 SMALL BREAK DESCRIPTIONS FOR MASS AND ENERGY TABLE 6.2.1-43 LARGE BREAK ANALYSIS - ASSOCIATED TIMES TABLE 6.2.1-44 SMALL BREAK ANALYSIS - SMALL SPLIT - ASSOCIATED TIMES TABLE 6.2.1-45 SAFETY INJECTION FLOW MINIMUM SAFEGUARDS TABLE 6.2.2-1 CONTAINMENT SPRAY PUMP/MOTOR DESIGN PARAMETERS TABLE 6.2.2-2 CONTAINMENT SPRAY HEAT EXCHANGER DESIGN PARAMETERS TABLE 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS TABLE 6.2.3-1 DUAL CONTAINMENT CHARACTERISTICS TABLE 6.2.3-2 FAILURE MODES AND EFFECTS ANALYSIS EMERGENCY GAS TREATMENT SYSTEM TABLE 6.2.3-3 FAILURE MODES AND EFFECTS ANALYSIS FOR PASSIVE FAILURE FOR THE ABGTS TABLE 6.2.3-3 FAILURE MODES AND EFFECTS ANALYSIS FOR THE ABGTS TABLE 6.2.4-1 WATTS BAR NUCLEAR PLANT CONTAINMENT PENETRATIONS AND BARRIERS TABLE 6.2.4-1 WATTS BAR NUCLEAR PLANT CONTAINMENT PENETRATIONS AND BARRIERS (SHEET 65 OF 69)
TABLE 6.2.4-1 WATTS BAR NUCLEAR PLANT CONTAINMENT PENETRATIONS AND BARRIERS (SHEET 66 OF 69)
TABLE 6.2.4-1 WATTS BAR NUCLEAR PLANT CONTAINMENT PENETRATIONS AND BARRIERS (SHEET 67 OF 69)
List of Tables 6-xiii
WATTS BAR LIST OF TABLES Section Title TABLE 6.2.4-1 WATTS BAR NUCLEAR PLANT CONTAINMENT PENETRATIONS AND BARRIERS (SHEET 68 OF 69)
TABLE 6.2.4-1 WATTS BAR NUCLEAR PLANT CONTAINMENT PENETRATIONS AND BARRIERS (SHEET 69 OF 69)
TABLE 6.2.4-2 POSSIBLE BYPASS LEAKAGE PATHS TO THE AUXILIARY BUILDING TABLE 6.2.4-3 PREVENTION OF BYPASS LEAKAGE TO THE ATMOSPHERE TABLE 6.2.4-4 INSTRUMENT LINES PENETRATING PRIMARY CONTAINMENT TABLE 6.2.6-1 PENETRATIONS SUBJECTED TO TYPE B TESTING TABLE 6.2.6-2 CONTAINMENT ISOLATION VALVES SUBJECTED TO TYPE C TESTING TABLE 6.2.6-3 VALVES EXEMPTED FROM TYPE C LEAK TESTING TABLE 6.2.6-4 CONTAINMENT VESSEL PRESSURE AND LEAK TEST REACTOR BUILDING CONTAINMENT PENETRATION STATUS TABLE 6.3-1 EMERGENCY CORE COOLING SYSTEM COMPONENT PARAMETERS TABLE 6.3-2 MATERIALS EMPLOYED FOR EMERGENCY CORE COOLING SYSTEM COMPONENTS TABLE 6.3-3 SEQUENCE OF CHANGE-OVER OPERATION, INJECTION TO RECIRCULATION TABLE 6.3-3A EVALUATION OF TIME SEQUENCE ASSOCIATED WITH CHANGEOVER OPERATION FROM INJECTION TO RECIRCULATION TABLE 6.3-4 NORMAL OPERATING STATUS OF EMERGENCY CORE COOLING SYSTEM COMPONENTS FOR CORE COOLING TABLE 6.3-5 EMERGENCY CORE COOLING SYSTEM SHARED FUNCTIONS EVALUATION TABLE 6.3-6 MAXIMUM RECIRCULATION LOOP LEAKAGE EXTERNAL TO CONTAINMENT TABLE 6.3-7 DELETED BY AMENDMENT 85 TABLE 6.3-8 FAILURE MODES AND EFFECTS ANALYSIS FOR ACTIVE FAILURES FOR THE SAFETY INJECTION SYSTEM TABLE 6.3-9 FAILURE MODES AND EFFECTS ANALYSIS FOR THE SAFETY INJECTION SYSTEM (PASSIVE FAILURES RECIRC. MODE)
List of Tables 6-xiv
WATTS BAR LIST OF TABLES Section Title TABLE 6.3-10 PRINCIPAL ECCS VALVE POSITIONS TABLE 6.3-11 NORMALIZED DECAY HEAT TABLE 6.3-12 AVAILABLE NPSH DURING ECCS OPERATION TABLE 6.4-1 (SHEET 1 OF 1)
AIR LEAKAGE (EXFILTRATION) PATHS IN THE WATTS BAR MCRHS AREA CONTROL ROOM TABLE 6.4-2 (SHEET 1 OF 1)
AIR LEAKAGE (INFILTRATION) PATHS IN THE WATTS BAR MCRHS AREA CONTROL ROOM TABLE 6.5-1 REGULATORY GUIDE 1.52, REV. 2, SECTION APPLICABILITY FOR THE EMERGENCY GAS TREATMENT SYSTEM TABLE 6.5-2 REGULATORY GUIDE 1.52, REV. 2, SECTION APPLICABILITY FOR THE AUXILIARY BUILDING GAS TREATMENT SYSTEM TABLE 6.5-3 DELETED BY AMENDMENT 111 TABLE 6.5-4 REGULATORY GUIDE 1.52, REV. 2, SECTION APPLICABILITY FOR THE MAIN CONTROL ROOM AIR CLEANUP SUBSYSTEM TABLE 6.5-5 ESF AIR CLEANUP UNIT DATA TABLE 6.5-6 DELETED IN FSAR AMENDMENT 65 TABLE 6.5-7 PRIMARY CONTAINMENT OPERATION FOLLOWING A DBA TABLE 6.5-8 SECONDARY CONTAINMENT OPERATION FOLLOWING A DBA TABLE 6.7-1 WALL PANEL DESIGN LOADS(1)
TABLE 6.7-2 ICE BASKET LOAD
SUMMARY
MINIMUM TEST LOADS TABLE 6.7-3
SUMMARY
OF STRESSES IN BASKET DUE TO DESIGN LOADS TABLE 6.7-4 ICE BASKET MATERIAL MINIMUM YIELD STRESS TABLE 6.7-5 ALLOWABLE STRESS LIMITS (D + OBE) FOR ICE BASKET MATERIALS TABLE 6.7-6 ALLOWABLE STRESS LIMITS (D + SSE), (D + DBA) FOR ICE BASKET MATERIALS TABLE 6.7-7 ALLOWABLE STRESS LIMITS (D + SSE + DBA) FOR ICE BASKET MATERIALS TABLE 6.7-8 ICE BASKET CLEVIS PIN STRESS
SUMMARY
TABLE 6.7-9 ICE BASKET MOUNTING BRACKET ASSEMBLY STRESS
SUMMARY
TABLE 6.7-10 ICE BASKET PLATE STRESS
SUMMARY
TABLE 6.7-11 ICE BASKET V-BOLT STRESS
SUMMARY
List of Tables 6-xv
WATTS BAR LIST OF TABLES Section Title TABLE 6.7-12 ICE BASKET - BASKET END STRESS
SUMMARY
TABLE 6.7-13 ICE BUCKET COUPLING SCREW STRESS
SUMMARY
3 INCH ELEVATION(1)
TABLE 6.7-14 ICE BUCKET COUPLING SCREW STRESS
SUMMARY
12 FOOT ELEVATION(1)
TABLE 6.7-15 ICE BASKET COUPLING SCREW STRESS
SUMMARY
24 FOOT ELEVATION(1)
TABLE 6.7-16 ICE BUCKET COUPLING SCREW STRESS
SUMMARY
36 FOOT ELEVATION(1)
TABLE 6.7-17 CRANE AND RAIL ASSEMBLY DESIGN LOADS TABLE 6.7-18 REFRIGERATION SYSTEM PARAMETERS TABLE 6.7-18 REFRIGERATION SYSTEM PARAMETERS CONTINUED TABLE 6.7-19 LOWER INLET DOOR DESIGN PARAMETERS AND LOADS TABLE 6.7-20 DESIGN LOADS AND PARAMETERS TOP DECK TABLE 6.7-21
SUMMARY
OF RESULTS UPPER BLANKET DOOR STRUCTURAL ANALYSIS - LOCA TABLE 6.7-22 DESIGN LOADS AND PARAMETERS INTERMEDIATE DECK TABLE 6.7-23
SUMMARY
OF WALTZ MILL TESTS TABLE 6.7-24 ICE CONDENSER RTDS TABLE 6.7-25 ICE CONDENSER ALLOWABLE LIMITS (1)
TABLE 6.7-26 SELECTION OF STRUCTURAL STEELS IN RELATION TO PREVENTION OF NON-DUCTILE FRACTURE OF ICE CONDENSER COMPONENTS TABLE 6.7-27
SUMMARY
OF WATTS BAR LOADS - TANGENTIAL CASE OBTAINED USING THE TWO-MASS DYNAMIC MODEL TABLE 6.7-28
SUMMARY
OF WATTS BAR LOADS - RADIAL CASE OBTAINED USING THE TWO-MASS DYNAMIC MODEL TABLE 6.7-29
SUMMARY
OF LOAD RESULTS OF FIVE NON-LINEAR DYNAMIC MODELS TABLE 6.7-30
SUMMARY
OF PARAMETERS USED IN THE SEISMIC ANALYSIS List of Tables 6-xvi
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.1-1 DELETED BY AMENDMENT 97 FIGURE 6.2.1-1 CONTAINMENT PRESSURE VERSUS TIME FIGURE 6.2.1-2A UPPER COMPARTMENT TEMPERATURE VERSUS TIME FIGURE 6.2.1-2B LOWER COMPARTMENT TEMPERATURE VERSUS TIME FIGURE 6.2.1-3 ACTIVE AND INACTIVE SUMP TEMPERATURE TRANSIENTS FIGURE 6.2.1-4 MELTED ICE MASS TRANSIENT FIGURE 6.2.1-4A COMPARISON OF CONTAINMENT PRESSURE VERSUS ICE MELT FIGURE 6.2.1-5 PLAN AT EQUIPMENT ROOMS ELEVATION FIGURE 6.2.1-6 CONTAINMENT SECTION VIEW FIGURE 6.2.1-7 PLAN VIEW AT ICE CONDENSER ELEVATION ICE CONDENSER COMPARTMENTS FIGURE 6.2.1-8 LAYOUT OF CONTAINMENT SHELL FIGURE 6.2.1-9 TMD CODE NETWORK FIGURE 6.2.1-10 UPPER AND LOWER COMPARTMENT PRESSURE TRANSIENT FOR WORST CASE BREAK COMPARTMENT (ELEMENT 1) HAVING A DEHL BREAK FIGURE 6.2.1-11 UPPER AND LOWER COMPARTMENT PRESSURE TRANSIENT FOR WORST CASE BREAK COMPARTMENT (ELEMENT 1) HAVING A DECL BREAK.
FIGURE 6.2.1-12 ILLUSTRATION OF CHOKED FLOW CHARACTERISTICS FIGURE 6.2.1-13 SENSITIVITY OF PEAK PRESSURE TO AIR COMPRESSION RATIO FIGURE 6.2.1-14 STEAM CONCENTRATION IN A VERTICAL DISTRIBUTION CHANNEL FIGURE 6.2.1-15 PEAK COMPRESSION PRESSURE VERSUS COMPRESSION RATIO FIGURE 6.2.1-16 PEAK COMPARTMENT PRESSURE VERSUS BLOWDOWN RATE FIGURE 6.2.1-17 SENSITIVITY OF PEAK COMPRESSION PRESSURE TO DECK BYPASS FIGURE 6.2.1-18 PRESSURE INCREASE VERSUS DECK AREA FROM DECK LEAKAGE TESTS FIGURE 6.2.1-19 ENERGY RELEASE AT TIME OF COMPRESSION PEAK PRESSURE FROM List of Figures 6-xvii
WATTS BAR LIST OF FIGURES Section Title FULL-SCALE SECTION TESTS WITH 1-FOOT DIAMETER BASKETS FIGURE 6.2.1-20 PRESSURE INCREASE VERSUS DECK AREA FROM DECK LEAKAGE TESTS FIGURE 6.2.1-21 DELETED BY AMENDMENT 97 FIGURE 6.2.1-22 DELETED BY AMENDMENT 97 FIGURE 6.2.1-23 DELETED BY AMENDMENT 97 FIGURE 6.2.1-24 DELETED BY AMENDMENT 97 FIGURE 6.2.1-25 DELETED BY AMENDMENT 97 FIGURE 6.2.1-26 DELETED BY AMENDMENT 97 FIGURE 6.2.1-27 CONTAINMENT MODEL SCHEMATIC.
FIGURE 6.2.1-28 REACTOR CAVITY TMD NETWORK.
FIGURE 6.2.1-29 REACTOR VESSEL ANNULUS FIGURE 6.2.1-30 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-31 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-32 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-33 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-34 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-35 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-36 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-37 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-38 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-39 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-40 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
List of Figures 6-xviii
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.2.1-41 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-42 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-43 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-44 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-45 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-46 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-47 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-48 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-49 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-50 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-51 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-52 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-53 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-54 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-55 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-56 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-57 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-58 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-59 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
List of Figures 6-xix
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.2.1-60 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-61 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-62 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-63 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-64 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-65 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-66 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-67 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-68 127 SQUARE INCH COLD LEG BREAK (REACTOR CAVITY ANALYSIS)
FIGURE 6.2.1-69 COMPARTMENT TEMPERATURE 1.4 FT2/LOOP, 100.6% POWER AFW RUNOUT PROTECTION FAILURE FIGURE 6.2.1-70 LOWER COMPARTMENT PRESSURE 1.4 FT2 LOOP, 100.6%
POWER AFW RUNOUT PROTECTION FAILURE FIGURE 6.2.1-71 COMPARTMENT TEMPERATURE 0.35 FT2 SPLIT, 30% POWER AFW RUNOUT PROTECTION FAILURE FIGURE 6.2.1-72 LOWER COMPARTMENT PRESSURE 0.35 FT2 SPLIT, 30%
POWER AFW RUNOUT PROTECTION FAILURE FIGURE 6.2.1-73 COMPARTMENT TEMPERATURE 0.6 FT2 SPLIT, 30% POWER AFW RUNOUT PROTECTION FAILURE FIGURE 6.2.1-74 LOWER COMPARTMENT PRESSURE 0.6 FT2 SPLIT, 30%
POWER AFW RUNOUT PROTECTION FAILURE FIGURE 6.2.1-75 MAXIMUM REVERSE PRESSURE DIFFERENTIAL MODEL FIGURE 6.2.1-76 MAXIMUM REVERSE PRESSURE DIFFERENTIAL UPPER AND LOWER COMPARTMENT PRESSURES FIGURE 6.2.1-77 MAXIMUM REVERSE PRESSURE DIFFERENTIAL UPPER AND LOWER COMPARTMENT TEMPERATURES FIGURE 6.2.1-78 MAXIMUM REVERSE PRESSURE DIFFERENTIAL UPPER TO LOWER COMPARTMENT FLOWRATES List of Figures 6-xx
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.2.1-79 MAXIMUM REVERSE PRESSURE DIFFERENTIAL CASE 6 UPPER AND LOWER COMPARTMENT PRESSURES FIGURE 6.2.1-80 MAXIMUM REVERSE PRESSURE DIFFERENTIAL CASE 6 UPPER AND LOWER COMPARTMENT TEMPERATURES FIGURE 6.2.1-81 STEAM GENERATOR ENCLOSURE NODALIZATION FIGURE 6.2.1-82 FLOW PATHS FOR TMD STEAM GENERATOR ENCLOSURE SHORT-TERM PRESSURE ANALYSIS FIGURE 6.2.1-83 PRESSURE TRANSIENT BETWEEN BREAK ELEMENT AND UPPER COMPARTMENT (STEAM GENERATOR ENCLOSURE ANALYSIS)
FIGURE 6.2.1-84 DIFFERENTIAL PRESSURE TRANSIENT ACROSS THE STEAM GENERATOR VESSEL (STEAM GENERATOR ENCLOSURE ANALYSIS)
FIGURE 6.2.1-85 DIFFERENTIAL PRESSURE TRANSIENT ACROSS THE STEAM GENERATOR VESSEL (STEAM GENERATOR ENCLOSURE ANALYSIS)
FIGURE 6.2.1-86 PRESSURE VERSUS TIME FOR THE BREAK ELEMENT (STEAM GENERATOR ENCLOSURE ANALYSIS)
FIGURE 6.2.1-86A UPPER COMPARTMENT PRESSURE VERSUS TIME (STEAM GENERATOR ENCLOSURE ANALYSIS)
FIGURE 6.2.1-87 NODALIZATION PRESSURE ENCLOSURE ANALYSIS FIGURE 6.2.1-88 PRESSURE TRANSIENT BETWEEN BREAK ELEMENT AND UPPER COMPARTMENT (PRESSURIZER ENCLOSURE ANALYSIS)
FIGURE 6.2.1-89 PRESSURE DIFFERENTIAL ACROSS THE PRESSURIZER VESSEL (PRESSURIZER ENCLOSURE ANALYSIS)
FIGURE 6.2.1-90 PRESSURE DIFFERENTIAL ACROSS THE PRESSURIZER VESSEL (PRESSURIZER ENCLOSURE ANALYSIS)
FIGURE 6.2.1-91 PRESSURE DIFFERENTIAL ACROSS THE PRESSURIZER VESSEL (PRESSURIZER ENCLOSURE ANALYSIS)
FIGURE 6.2.1-92 PRESSURE VERSUS TIME FOR THE BREAK ELEMENT (PRESSURIZER ENCLOSURE ANALYSIS)
FIGURE 6.2.2-1 POWERHOUSE UNITS 1 & 2 MECHANICAL FLOW DIAGRAM CONTAINMENT SPRAY SYSTEM FIGURE 6.2.2-2 CONTAINMENT SPRAY PUMP PERFORMANCE CURVES List of Figures 6-xxi
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.2.2-3 REACTOR BLDGS. UNITS 1 & 2 MECHANICAL CONTAINMENT SPRAY SYSTEM PIPING PLAN OF SPRAY PATTERNS FROM C.S. LOOP HEADER A
FIGURE 6.2.2-4 POWERHOUSE-AUXILIARY & REACTOR BLDGS UNITS 1 & 2 MECHANICAL CONTAINMENT SPRAY SYSTEM PIPING FIGURE 6.2.2-5 REACTOR BLDGS. UNITS 1 & 2 MECHANICAL CONTAINMENT SPRAY SYSTEM PIPING PLAN OF SPRAY PATTERNS FROM C.S. LOOP HEADER B FIGURE 6.2.2-6 REACTOR BLDGS. UNITS 1 & 2 MECHANICAL CONTAINMENT SPRAY SYSTEM PIPING SECTION OF SPRAY PATTERNS FROM C.S. LOOP HEADER B FIGURE 6.2.3-1 TYPICAL MECHANICAL PENETRATION SEALS FIGURE 6.2.3-2 TYPICAL PURGE PENETRATION ARRANGEMENT FIGURE 6.2.3-3 TYPICAL ELECTRICAL PENETRATIONS FIGURE 6.2.3-4 AUXILIARY BUILDING ISOLATION BARRIER FIGURE 6.2.3-5 AUXILIARY BUILDING ISOLATION BARRIER FIGURE 6.2.3-6 AUXILIARY BUILDING ISOLATION BARRIER FIGURE 6.2.3-7 AUXILIARY BUILDING ISOLATION BARRIER FIGURE 6.2.3-8 AUXILIARY BUILDING ISOLATION BARRIER FIGURE 6.2.3-9 AUXILIARY BUILDING ISOLATION BARRIER FIGURE 6.2.3-10 AUXILIARY BUILDING ISOLATION BARRIER FIGURE 6.2.3-11 REACTOR BUILDING - UNITS 1 & 2 FLOW DIAGRAM -
HEATING AND VENTILATION AIR FLOW FIGURE 6.2.3-12 POWERHOUSE UNITS 1 & 2 ELECTRICAL LOGIC DIAGRAM -
EMERGENCY GAS TREATMENT SYSTEM FIGURE 6.2.3-13 POWERHOUSE UNITS 1 & 2 ELECTRICAL LOGIC DIAGRAM -
EMERGENCY GAS TREATMENT FIGURE 6.2.3-14 POWERHOUSE UNIT 1 ELECTRICAL LOGIC DIAGRAM -
EMERGENCY GAS TREATMENT FIGURE 6.2.3-15 POWERHOUSE UNITS 1 & 2 ELECTRICAL CONTROL DIAGRAM
- EMERGENCY GAS TREATMENT SYSTEM FIGURE 6.2.3-15-SH-A POWERHOUSE UNIT 2 ELECTRICAL CONTROL DIAGRAM -
EMERGENCY GAS TREATMENT FIGURE 6.2.3-16 POWERHOUSE UNITS 1 & 2 AUXILIARY BUILDING -FLOW DIAGRAM -HEATING & VENTILATING AIR FLOW List of Figures 6-xxii
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.2.3-17A POST-ACCIDENT ANNULUS PRESSURE AND VENT FLOW RATE FIGURE 6.2.3-17 POST-ACCIDENT ANNULUS PRESSURE AND REACTOR UNIT VENT FLOW RATE TRANSIENTS FIGURE 6.2.3-18 REACTOR BUILDING UNITS 1 & 2 MECHANICAL HEATING AND VENTILATING FIGURE 6.2.3-19 REACTOR BUILDING UNITS 1 & 2 MECHANICAL HEATING, VENTILATION, AND AIR CONDITIONING FIGURE 6.2.4-1 TYPE 1, MAIN STEAM X-L3A, X-L3B, X-L3C, X-13D FIGURE 6.2.4-2 TYPE II, FEEDWATER X-12A, X-L2B, X-12C, X-12D FIGURE 6.2.4-3 TYPE III, RESIDUAL HEAT REMOVAL PUMP RETURN X-17, PUMP SUPPLY X-I07 FIGURE 6.2.4-4 TYPE IV AND V (TYPE IV SOCKET WELD ENDS, TYPE V BUTT WELD ENDS)
FIGURE 6.2.4-5 TYPE VI AND VII (TYPE VI FOR SOCKET WELD SS PROCESS LINES, TYPE VII FOR BUTT WELD SS PROCESS LINES)
FIGURE 6.2.4-6 TYPE VIII, FOR BUTT WELD C.S. PROCESS LINES FIGURE 6.2.4-7 TYPE IX, FOR SS PROCESS LINES FIGURE 6.2.4-8 TYPE X, INSTRUMENT PENETRATIONS FIGURE 6.2.4-9 TYPE XII, EMERGENCY SUMP FIGURE 6.2.4-10 TYPE XI, EMERGENCY SUMP FIGURE 6.2.4-11 TYPE XIII, VENTILATION DUCT PENETRATION FIGURE 6.2.4-12 TYPE XIV, EQUIPMENT HATCH FIGURE 6.2.4-13 TYPE XV, PERSONNEL ACCESS FIGURE 6.2.4-14 TYPE XVI, TRANSFER TUBE FIGURE 6.2.4-15 TYPE XVII, INCORE INSTRUMENTATION THIMBLE ASSEMBLY RENEWAL LINE FIGURE 6.2.4-16 TYPE XVIII, ICE BLOWING LINE FIGURE 6.2.4-17 TYPE XIX, ELECTRICAL PENETRATION FIGURE 6.2.4-17A TYPE XX FEEDWATER BYPASS PENETRATIONS X-8A, X-8B, X-8C, X-8D FIGURE 6.2.4-17B TYPE XXI, UPPER AND LOWER CONTAINMENT ERCW SUPPLY AND RETURN CCW FROM EXCESS LETDOWN HEAT EXCHANGER AND FROM PUMP ODOLERS List of Figures 6-xxiii
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.2.4-17C TYPE XXII MULTI LINE PENETRATION X-39 FIGURE 6.2.4-17D TYPE XXIII INSTRUMENT ROOM CHILLED H20 SUPPLY AND RETURN FIGURE 6.2.4-17E TYPE XXIV UHI X-L08, X-109 FIGURE 6.2.4-18 MECHANICAL CONTAINMENT PENETRATION FIGURE 6.2.4-19 POWERHOUSE REACTOR BUILDING UNIT 1 & 2 MECHANICAL SLEEVES-SHIELD BUILDING FIGURE 6.2.4-20 SCHEMATIC DIAGRAM OF LEAKAGE PATHS FIGURE 6.2.4-21 ELECTRICAL LOGIC DIAGRAM CONTAINMENT ISOLATION FIGURE 6.2.4-22A THROUGH 6.2.4-22II DELETED BY AMENDMENT 65 FIGURE 6.2.4-23 ICE BLOWING AND NEGATIVE RETURN LINES - BLIND FLANGE DETAILS FIGURE 6.2.5-1 DELETED BY AMENDMENT 95 FIGURE 6.2.5-2 DELETED BY AMENDMENT 62 FIGURE 6.2.5-3 POWERHOUSE REACTOR BUILDING UNITS 1 & 2 -
MECHANICAL HEATING, VENTILATING AND AIR CONDITIONING FIGURE 6.2.5-4 POWERHOUSE REACTOR BUILDING UNITS 1 & 2 -
MECHANICAL HEATING, VENTILATING AND AIR CONDITIONING FIGURE 6.2.5-5 POWERHOUSE REACTOR BUILDING UNITS 1 & 2 -
MECHANICAL HEATING, VENTILATION AND AIR CONDITIONING FIGURE 6.2.5-6 SAMPLE LOOP FLOW DIAGRAM FIGURE 6.2.5-7 DELETED BY AMENDMENT 95 FIGURE 6.2.5-7A DELETED BY AMENDMENT 95 FIGURE 6.2.5-8 IGNITER LOCATIONS - LOWER COMPARTMENT AND DEAD ENDED COMPARTMENTS FIGURE 6.2.5-9 IGNITER LOCATIONS - LOWER COMPARTMENTS FIGURE 6.2.5-10 IGNITER LOCATIONS - UPPER PLENUM AND UPPER COMPARTMENTS FIGURE 6.2.5-11 IGNITER LOCATIONS - DOME FIGURE 6.2.5-12 IGNITER LOCATIONS - ELEVATION FIGURE 6.3-1-1 POWERHOUSE UNIT 1 SAFETY INJECTION SYSTEM - FLOW DIAGRAM List of Figures 6-xxiv
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.3-1-2 POWERHOUSE UNIT 1 & 2 ELECTRICAL CONTROL DIAGRAM
- SAFETY INJECTION SYSTEM FIGURE 6.3-1-2-SH-A POWERHOUSE UNIT 1 ELECTRICAL CONTROL DIAGRAM -
SAFETY INJECTION SYSTEM FIGURE 6.3-1-3 POWERHOUSE UNIT 1 ELECTRICAL CONTROL DIAGRAM SAFETY INJECTION FIGURE 6.3-1-3-SH-A POWERHOUSE UNIT 2 ELECTRICAL CONTROL DIAGRAM -
SAFETY INJECTION FIGURE 6.3-1-3-SH-B POWERHOUSE UNIT 1 ELECTRICAL CONTROL DIAGRAM -
SAFETY INJECTION FIGURE 6.3-2 UNIT 2 - PERFORMANCE CURVES FOR THE RESIDUAL HEAT REMOVAL PUMPS FIGURE 6.3-3 PERFORMANCE CURVES FOR THE SAFETY INJECTION PUMPS FIGURE 6.3-4 PERFORMANCE CURVES FOR THE CHARGING PUMPS FIGURE 6.3-5 SHEETS 1 AND 2, DELETED BY AMENDMENT 63 FIGURE 6.3-6 CONTAINMENT SUMP FIGURE 6.3-6A CONTAINMENT SUMP FIGURE 6.5-1 ICE CONDENSER FIGURE 6.7-1 ISOMETRIC OF ICE CONDENSER FIGURE 6.7-2 FLOOR STRUCTURE FIGURE 6.7-3 WEAR SLAB TOP SURFACE AREA SHOWING TYPICAL COOLANT PIPING LAYOUT FIGURE 6.7-4 LATTICE FRAME ORIENTATION FIGURE 6.7-5 LOAD DISTRIBUTION FOR TANGENTIAL SEISMIC AND BLOWDOWN LOADS IN ANALYTICAL MODEL FIGURE 6.7-6 LATTICE FRAME FIGURE 6.7-7 LATTICE FRAME ANALYSIS MODEL FIGURE 6.7-8 TYPICAL BOTTOM ICE BASKET ASSEMBLY FIGURE 6.7-9 COMBINATIONS OF CONCENTRIC AXIAL LOAD AND DISTRIBUTION LOAD THAT WILL CAUSE FAILURE OF A PERFORATED METAL ICE CONDENSER BASKET MATERIAL FIGURE 6.7-10 CRANE ASSEMBLY FIGURE 6.7-11 CRANE RAIL ASSEMBLY FIGURE 6.7-12 REFRIGERANT CYCLE DIAGRAM List of Figures 6-xxv
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.7-13 GLYCOL CYCLE TO EACH CONTAINMENT FIGURE 6.7-14 SCHEMATIC FLOW DIAGRAMS OF AIR COOLING CYCLE FIGURE 6.7-15 AIR HANDLING UNIT SUPPORT STRUCTURE FIGURE 6.7-16 FLOW AREA - PRESSURE DIFFERENTIAL FIGURE 6.7-17 LOWER INLET DOOR ASSEMBLY FIGURE 6.7-18 DETAILS OF LOWER INLET DOOR SHOWING HINGE, PROPORTIONING MECHANISM LIMIT SWITCHES AND SEALS FIGURE 6.7-19 INLET DOOR FRAME ASSEMBLY FIGURE 6.7-20 INLET DOOR PANEL ASSEMBLY FIGURE 6.7-21 LOWER INLET DOOR SHOCK ABSORBER ASSEMBLY FIGURE 6.7-22 FOUR LOOP ICE CONDENSER LOWER SUPPORT STRUCTURE CONCEPTUAL PLAN AND SECTIONS FIGURE 6.7-23 FOUR LOOP ICE CONDENSER LOWER SUPPORT STRUCTURE GENERAL ASSEMBLY FIGURE 6.7-24 ANTS MODEL ASSEMBLY FIGURE 6.7-25 FINITE ELEMENT MODEL OF PORTAL FRAME FIGURE 6.7-26 SCHEMATIC DIAGRAM OF FORCES APPLIED TO THREE PIER LOWER SUPPORT STRUCTURE FIGURE 6.7-27 FORCE TRANSIENT HOT LEG BREAK FIGURE 6.7-28 DLF SPECTRA HOT LEG BREAK FORCE TRANSIENT FIGURE 6.7-29 TOP DECK TEST ASSEMBLY FIGURE 6.7-30 DETAILS OF TOP DECK DOOR ASSEMBLY FIGURE 6.7-31 INTERMEDIATE DECK DOOR ASSEMBLY FIGURE 6.7-32 AIR DISTRIBUTION DUCT FIGURE 6.7-33 AIR DISTRIBUTION DUCT FIGURE 6.7-34 PHASE DIAGRAM FOR NA2 B4 07.10 H2O/WATER SYSTEM AT ONE ATMOSPHERE FIGURE 6.7-35 ICE BED COMPACTION VERSUS TIME FIGURE 6.7-36 TEST ICE BED COMPACTION VERSUS ICE BED HEIGHT FIGURE 6.7-37 TOTAL ICE COMPACTION VERSUS ICE BED HEIGHT FIGURE 6.7-38 ICE CONDENSER RTD LOCATION FIGURE 6.7-39 BLOCK DIAGRAM ICE CONDENSER TEMPERATURE MONITORING SYSTEM FIGURE 6.7-40 DOOR MONITORING ZONES List of Figures 6-xxvi
WATTS BAR LIST OF FIGURES Section Title FIGURE 6.7-41 POWERHOUSE UNIT 1 WIRING DIAGRAMS ICE CONDENSER SYSTEM SCHEMATIC DIAGRAMS FIGURE 6.7-42 DELETED BY AMENDMENT 89 FIGURE 6.7-43 DELETED BY AMENDMENT 89 FIGURE 6.7-44 MODEL OF HORIZONTAL LATTICE FRAME STRUCTURE FIGURE 6.7-45 GROUP OF SIX INTERCONNECTED LATTICE FRAMES FIGURE 6.7-46 LATTICE FRAME LCE BASKET GAP FIGURE 6.7-47 TYPICAL DISPLACEMENT TIME HISTORIES FOR 12-FOOT BASKET WITH END SUPPORTS - PLUCK TEST FIGURE 6.7-48 NON LINEAR DYNAMIC MODEL FIGURE 6.7-49 3-MASS TANGENTIAL ICE BASKET MODEL FIGURE 6.7-50 9-MASS RADIAL ICE BASKET MODEL FIGURE 6.7-51 48-FOOT BEAM MODEL FIGURE 6.7-52 PHASING MASS MODEL OF ADJACENT LATTICE FRAME BAYS FIGURE 6.7-53 PHASING STUDY MODEL, 1 LEVEL LATTICE FRAME 300 DEGREES NON-LINEAR MODEL FIGURE 6.7-54 TYPICAL CRANE WALL DISPLACEMENT FIGURE 6.7-55 TYPICAL ICE BASKET DISPLACEMENT RESPONSE FIGURE 6.7-56 TYPICAL ICE BASKET IMPACT FORCE RESPONSE FIGURE 6.7-57 TYPICAL CRANE WALL PANEL LOAD RESPONSE FIGURE 6.7-58 WALL PANEL DESIGN LOAD DISTRIBUTION OBTAINED USING THE 48-FOOT BEAM MODEL TANGENTIAL CASE FIGURE 6.7-59 WALL PANEL DESIGN LOAD DISTRIBUTION OBTAINED USING THE 48-FOOT BEAM MODEL RADIAL CASE List of Figures 6-xxvii
WATTS BAR LIST OF FIGURES Section Title THIS PAGE INTENTIONALLY BLANK List of Figures 6-xxviii
WATTS BAR WBNP-112 06-1_Part_01_of_02_LTR.pdf 6.0 ENGINEERED SAFETY FEATURES 6.1 ENGINEERED SAFETY FEATURE MATERIALS 6.1.1 Metallic Materials 6.1.1.1 Materials Selection and Fabrication Typical material specifications used for the principal pressure retaining applications in components in the Engineered Safety Features (ESF) are listed inTable 5.2-9. All materials utilized are procured in accordance with the material specification requirements of the ASME Boiler and Pressure Vessel Code,Section III, plus applicable and appropriate Addenda and Code Cases.
The welding materials used for joining the ferritic base materials of the ESF conform to, or are equivalent to, ASME Material Specifications SFA 5.1, 5.2, 5.5, 5.17, 5.18, and 5.20. The welding materials used for joining nickel-chromium-iron alloy in similar base material combination and in dissimilar ferritic or austenitic base material combination conform to ASME Material Specifications SFA 5.11 and 5.14. The welding materials used for Joining the austenitic stainless steel base materials conform to ASME Material Specifications SFA 5.4 and 5.9. These materials are tested and qualified to the requirements of the ASME Code,Section III and Section IX rules and are used in procedures which have been qualified to these same rules. The methods utilized to control delta ferrite content in austenitic stainless steel weldments are discussed in Section 5.2.5.7.
The parts of components in contact with borated water are fabricated of or clad with austenitic stainless steel or equivalent corrosion resistant material [Ref. 4]. The integrity of the safety-related components of the ESF is maintained during all stages of component manufacture. Austenitic stainless steel is utilized in the final heat treated condition as required by the respective ASME Code Section II material specification for the particular type or grade of alloy. Furthermore, it is required that austenitic stainless steel materials used in the ESF components be handled, protected, stored, and cleaned according to recognized and accepted methods which are designed to minimize contamination which could lead to stress corrosion cracking. The rules covering these controls are stipulated in Westinghouse process specifications, which are discussed in Section 5.2.5.1. Additional information concerning austenitic stainless steel, including the avoidance of sensitization and the prevention of intergranular attack, can be found in Section 5.2.5. No cold worked austenitic stainless steels having yield strengths greater than 90,000 psi are used for components of the ESF within the Westinghouse standard scope.
Westinghouse supplied components within the containment that would be exposed to core cooling water and containment sprays in the event of a loss-of-coolant accident utilize materials listed in Table 5.2-9. These components are manufactured primarily of stainless steel or other corrosion resistant, high temperature material. The integrity of the materials of construction for ESF equipment when exposed to post design basis accident (DBA) conditions has been evaluated. Post-DBA conditions were ENGINEERED SAFETY FEATURE MATERIALS 6.1-1
WATTS BAR WBNP-112 conservatively represented by test conditions. The test program[1] performed by Westinghouse considered spray and core cooling solutions of the design chemical compositions, as well as the design chemical compositions contaminated with corrosion and deterioration products which may be transferred to the solution during recirculation. The effects of sodium (free caustic), chlorine (chloride), and fluorine (fluoride) on austenitic stainless steels were considered. Based on the results of this investigation, as well as testing by ORNL and others, the behavior of austenitic stainless steels in the post-DBA environment will be very acceptable. No cracking is anticipated on any equipment even in the presence of postulated levels of contaminants, provided the core cooling and spray solution pH is maintained at an adequate level. The inhibitive properties of alkalinity (hydroxyl ion) against chloride cracking and the inhibitive characteristic of boric acid on fluoride cracking have been demonstrated. Note that qualified coatings inside primary containment located within the zone of influence are assumed to fail for the analysis in the event of a loss-of-coolant accident. The zone of influence for qualified coatings is defined as a spherical zone with a radius of 10 times the break diameter. Coatings on exposed surfaces outside the zone of influence within the containment are not subject to breakdown under exposure to the spray solution and can withstand the temperature and pressure expected in the event of a loss-of-coolant accident.
6.1.1.2 Composition, Compatibility, and Stability of Containment and Core Spray Coolants The vessels used for storing ESF coolants include the accumulators and the refueling water storage tank.
The accumulators are carbon steel clad with austenitic stainless steel [Ref. 4].
Because of the corrosion resistance of these materials, significant corrosive attack on the storage vessels is not expected.
The accumulators are vessels filled with borated water and pressurized with nitrogen gas. The nominal boron concentration, as boric acid, is 3150 ppm. Samples of the solution in the accumulators are taken periodically for checks of boron concentration.
Principal design parameters of the accumulators are listed in Table 6.3-1.
The refueling water storage tank is a source of borated cooling water for injection. The nominal boron concentration, as boric acid, is 3200 ppm . The temperature of the refueling water is maintained above the solubility limit for the maximum boron concentration. Principal design parameters of the refueling water storage tank are given in Section 9.2.7.
The ice in the ice condenser is borated by adding sodium tetraborate to the ice. The aqueous solution resulting from the melted ice has a nominal boron concentration of 1900 +100 ppm. In the event of an accident, this solution would be delivered to the containment sump. Containment sump pH is also controlled by the sodium tetraborate in the ice. The pH of the ice is maintained between 9.0 and 9.5, which results in a sump pH of at least 7.5.
6.1-2 ENGINEERED SAFETY FEATURE MATERIALS
WATTS BAR WBNP-112 Information concerning hydrogen release by the corrosion of containment metals and the control of the hydrogen and combustible gas concentrations within the containment following a LOCA is discussed in Section 6.2.5.
6.1.2 Organic Materials For paints and coatings inside containment, the conformance with Regulatory Guide 1.54 is described in Section 6.1.4.
Organic materials within the primary containment are identified and quantified according to the following categories: electrical insulation, surface coatings, miscellaneous ALARA (catch basin), containment and shielding (lead blankets), ice condenser equipment, and identification tags for valves and instruments. There is no asphalt inside containment. There is a small amount of wood (roughly 215 lbs) located inside the ice condenser. The effects of elastomers and plastic on hydrogen generation have been evaluated and determined to be inconsequential. Therefore, the quantities identified below are considered historical and need not be revised due to design changes.
The information in this section is based on a single reactor unit.
6.1.2.1 Electrical Insulation The typical types of electrical cable insulation/jacket material that are utilized within the primary containment are: silcon rubber, polyethylene, ethylene rubber, chlorosulfonated polyethlene, polylefin, cross linked polyethlene, kapton. These materials are not significant contributors to hydrongen generation during a design basis accident (approximately 28,000 lbs).
6.1.2.2 Surface Coatings Material Mass, lbs Concrete Surfaces:
Epoxy 2070 Phenolic-epoxy 300 Steel Surfaces:
Phenolic-epoxy 1810 Steel surfaces are undercoated with approximately 85% zinc in a silicate binder (carbozinc 11), or epoxy, such as Amerlock 400.
Protective coatings for use in the reactor containment have been evaluated as to their suitability in post-DBA conditions. Tests have shown that the epoxy and modified phenolic systems are the most desirable of the generic types evaluated for in-containment use. This evaluation considered resistance to high temperature and chemical conditions anticipated following a LOCA, as well as high radiation resistance
[Ref. 2]. Coating systems qualified as CSL-1, for one plant may be used by the other ENGINEERED SAFETY FEATURE MATERIALS 6.1-3
WATTS BAR WBNP-112 plants provided the applicable DBA requirements for the area where it is to be used are enveloped by the qualification testing system. These requirements include but are not limited to temperature, pressure, radiation and spray solution.
6.1.2.3 Ice Condenser Equipment Material Mass, lbs Lower Door Seals (Styrene butadiene) 530 Equipment Access Door Seals (Natural rubber) 5 Vent curtain (Laminated mylar) 5 Ice Condenser Seal:
Natural Rubber 600 Nylon 360 Miscellaneous Washers:
Noryl SEIOO (phenylene oxide) 50 Gasketing Material:
Neoprene 5060 Drain Line Expansion Joint 6.1.2.4 Identification Tags Material Mass, lbs Valves:
ABS (acrylonitrile-butadiene-styrene) 50 Instruments:
ABS (acylonitrile-butadiene-styrene) 30 6.1.2.5 Valves and Instruments within Containment Material Mass, lbs Diaphragms, O-Rings, Solenoid Seals:
Buna-N (acrylonitrile-Butadiene) 130 6.1-4 ENGINEERED SAFETY FEATURE MATERIALS
WATTS BAR WBNP-112 6.1.2.6 Heating and Ventilating Door Seals Material Mass, lbs Neoprene (chloroprene) 100 6.1.2.7 Miscellaneous Material Mass, lbs Catch Basins (polyethylene) 100 Lead Shielding Blankets (Hypalon, Vinyl, 1200 Methyllpolysiloxance) 6.1.3 Post-Accident Chemistry Following a LOCA, the emergency core cooling solution recirculated in containment is composed of boric acid (H3BO3) from the reactor coolant, refueling water storage tank (RWST), cold leg accumulators and affected injection piping, lithium hydroxide (LiOH) from the reactor coolant and sodium tetraborate (Na2B4O7) from the ice in the ice condenser.
6.1.3.1 Boric Acid, H3BO3 Boric acid up to a maximum concentration of 3300 ppm boron, can be found in the reactor coolant loop (4 loops, reactor vessel, pressurizer), and boric acid at a maximum concentration of 3300 ppm boron is found in the cold leg injection accumulators, the refueling water storage tank, and in associated piping. This limit may be exceeded during Mode 6 operation. These subsystems, when at maximum volume, represent a total mass of boric acid in the amount of 93,928 pounds.
6.1.3.2 Lithium Hydroxide Lithium Hydroxide at a maximum concentration of 7.6 ppm lithium is found in the reactor coolant system for pH control.
6.1.3.3 Sodium Tetraborate Sodium tetraborate is an additive in the ice stored in the ice condenser for the purpose of maintaining containment sump pH of at least 7.5 after all the ice has melted.
The minimum amount of ice assumed in the Post-LOCA sump pH analysis is 2.26 x 106 lbs [Ref. 3]. Boric acid and NaOH are formed during ice melt following a LOCA according to the following equation:
Na 2 B 4 O 7 + 7H 2 O 2NaOH + 4H 3 BO 3 ENGINEERED SAFETY FEATURE MATERIALS 6.1-5
WATTS BAR WBNP-112 6.1.3.4 Final Post-Accident Chemistry The final post-accident sump pH is greater than 7.5. The estimated sump pH versus time calculation indicates that the post-LOCA sump pH remains within the allowable range of 7.5 to 10.0 for the duration of the event.
6.1.4 Degree of Compliance with Regulatory Guide 1.54 for Paints and Coatings Inside Containment TVA is committed to adhere to Appendix B of 10 CFR 50 and ANSI N45.2 as required to produce a quality end product. Basically, it is TVA's position that the Quality Assurance Program (QA) for protective coatings inside the containment should control four activities in the coating program. The four major areas to be controlled are:
(1) The coating material itself, by extending requirements on the manufacturing process and qualification of coating systems through the use of applicable portions of ANSI Standards N101.2 and N512.
(2) The preparation of the surface to which coatings are to be applied.
(3) The inspection process.
(4) The application of the coating systems.
All four of these controlled activities have appropriate documentation and records to meet Appendix B requirements.
TVA agrees with Regulatory Guide 1.54, except the endorsement to ANSI N101.4 in paragraph C.1.
TVA's protective coating application program within the containment is in conformance with Appendix B to 10 CFR 50 and ANSI N45.2. In addition, applicable provisions found in ANSI N101.4 have been incorporated into TVA surface preparation, coating application/inspection specifications, and coating QA procedures.
Unqualified/uncontrolled coatings are accounted for and maintained within the limits specified in the analysis for containment coatings and in the transport analysis for the zone of influence. The zone of influence is defined as that area at the water surface into which a falling paint particle does not settle to the bottom, but rather, is transported to the sump strainer assembly by the flow of water.
REFERENCES (1) WCAP-7803, "Behavior of Austenitic Stainless Steel in Post Hypothetical Loss of Coolant Environment."
(2) WCAP-7825, "Evaluation of Protective Coatings for Use in Reactor Containment."
6.1-6 ENGINEERED SAFETY FEATURE MATERIALS
WATTS BAR WBNP-112 (3) WBT-D-1413, Response to Comments on FSAR Mark-ups, dated January 7, 2010.
(4) TVAs letter to NRC dated July 30, 2003, Petition Pursuant to 10 CFR 2.206
- Reactor Coolant System Stainless Steel Cladding. (Unit 1)
ENGINEERED SAFETY FEATURE MATERIALS 6.1-7
WATTS BAR WBNP-112 Table 6.1-1 Deleted by Amendment 97 6.1-8 ENGINEERED SAFETY FEATURE MATERIALS
Deleted by Amendment 97 WATTS BAR ENGINEERED SAFETY FEATURE MATERIALS 6.1-9 Figure 6.1-1 Deleted by Amendment 97 WBNP-112
WATTS BAR WBNP-112 THIS PAGE INTENTIONALLY BLANK 6.1-10 ENGINEERED SAFETY FEATURE MATERIALS
WATTS BAR WBNP-112 6.2 CONTAINMENT SYSTEMS 6.2.1 Containment Functional Design 6.2.1.1 Design Bases 6.2.1.1.1 Primary Containment Design Bases The containment is designed to assure that an acceptable upper limit of leakage of radioactive material is not exceeded under design basis accident conditions. For purposes of integrity, the containment may be considered as the containment vessel and containment isolation system. This structure and system are directly relied upon to maintain containment integrity. The emergency gas treatment system and Reactor Building function to keep out-leakage minimal (the Reactor Building also serves as a protective structure), but are not factors in determining the design leak rate.
The containment is specifically designed to meet the intent of the applicable General Design Criteria listed in Section 3.1. This section, Chapter 3, and other portions of Chapter 6 present information showing conformance of design of the containment and related systems to these criteria.
The ice condenser is designed to limit the containment pressure below the design pressure for all reactor coolant pipe break sizes up to and including a double-ended severance. Characterizing the performance of the ice condenser requires consideration of the rate of addition of mass and energy to the containment as well as the total amounts of mass and energy added. Analyses have shown that the accident which produces the highest blowdown rate into a condenser containment will result in the maximum containment pressure rise; that accident is the double-ended guillotine or split severance of a reactor coolant pipe. The design basis accident for containment analysis based on sensitivity studies is therefore the double-ended guillotine severance of a reactor coolant pipe at the reactor coolant pump suction. Post-blowdown energy releases can also be accommodated without exceeding containment design pressure.
The functional design of the containment is based upon the following accident input source term assumptions and conditions:
(1) The design basis blowdown energy of 314.9 x 106 Btu and mass of 498.1 x 103 lb put into the containment. (See Section 6.2.1.3.6)
(2) A core power of 3411 MWt (plus 2% allowance for calorimetric error). (See Section 6.2.1.3.6)
Containment Functional Design 6.2.1-1
WATTS BAR WBNP-112 (3) The minimum engineered safety features are (i.e., the single failure criterion applied to each safety system) comprised of the following:
(a) The ice condenser which condenses steam generated during a LOCA, thereby limiting the pressure peak inside the containment (see Section 6.7).
(b) The containment isolation system which closes those fluid penetrations not serving accident-consequence limiting purposes (see Section 6.2.4).
(c) The containment spray system which sprays cool water into the containment atmosphere, thereby limiting the pressure peak (particularly in the long term - see Section 6.2.2).
(d) The emergency gas treatment system (EGTS) which produces a slightly negative pressure within the annulus, thereby precluding out-leakage and relieving the post-accident thermal expansion of air in the annulus (see Section 6.5.1).
(e) The air return fans which return air to the lower compartment (See Section 6.8).
Consideration is given to subcompartment differential pressure resulting from a design basis accident discussed in Sections 3.8.3.3, 6.2.1.3.9, and 6.2.1.3.4. If a design basis accident were to occur due to a pipe rupture in these relatively small volumes, the pressure would build up at a faster rate than in the containment, thus imposing a differential pressure across the wall of these structures.
Parameters affecting the assumed capability for post-accident pressure reduction are discussed in Section 6.2.1.3.3.
Three events that may result in an external pressure on the containment vessel have been considered:
(1) Rupture of a process pipe where it passes through the annulus.
(2) Inadvertent air return fan operation during normal operation.
(3) Inadvertent containment spray system initiation during normal operation.
The design of the guard pipe portion of hot penetrations is such that any process pipe leakage in the annulus is returned to the containment. All process piping which has potential for annulus pressurization upon rupture is routed through hot penetrations.
Section 6.2.4 discusses hot penetrations.
Inadvertent air return fan operation during normal operation opens the ice condenser lower inlet doors, which in turn, results in sounding an alarm in the MCR. Sufficient 6.2.1-2 Containment Functional Design
WATTS BAR WBNP-112 time exists for operator action to terminate fan operation prior to exceeding the containment design external pressure.
The logic and control circuits of the containment spray system are such that inadvertent containment spray would not take place with a single failure. The spray pump must start and the isolation valve must open before there can be any spray. In addition, the Watts Bar containment is so designed that even if an inadvertent spray occurs, containment integrity is preserved without the use of a vacuum relief.
The containment spray system is automatically actuated by a hi-hi containment pressure signal from the solid state protection system (SSPS). To prevent inadvertent automatic actuation, four comparator outputs, one from each protection set are processed through two coincidence gates. Both coincidence gates are required to have at least two high inputs before the output relays, which actuate the containment spray system, are energized. Separate output relays are provided for the pump start logic and discharge valve open logic. Additional protection is provided by an interlock between the pump and discharge valve, which requires the pump to be running before the discharge valve will automatically open.
Section 3.8.2 describes the structural design of the containment vessel. The containment vessel is designed to withstand a net external pressure of 2.0 psi. The containment vessel is designed to withstand the maximum expected net external pressure in accordance with ASME Boiler and Pressure and Vessel Code Section III, paragraph NE-7116.
6.2.1.2 Primary Containment System Design The containment consists of a containment vessel and a separate Shield Building enclosing an annulus. The containment vessel is a freestanding, welded steel structure with a vertical cylinder, hemispherical dome, and a flat circular base. The Shield Building is a reinforced concrete structure similar in shape to the containment vessel. The design of these structures is described in Section 3.8.
The design internal pressure for the containment is 13.5 psig, and the design temperature is 250°F. The design basis leakage rate is 0.25 weight percent/24 hr. The design methods to assure integrity of the containment internal structures and sub-compartments from accident pressure pulses are described in Section 3.8.
6.2.1.3 Design Evaluation 6.2.1.3.1 Primary Containment Evaluation (1) The leaktightness aspect of the secondary containment is discussed in Section 6.2.3. The primary containment's leaktightness does not depend on the operation of any continuous monitoring or compressor system. The leak testing of the primary containment and its isolation system is discussed in Section 6.2.6.
Containment Functional Design 6.2.1-3
WATTS BAR WBNP-112 (2) The acceptance criteria for the leaktightness of the primary containment are such that at containment design pressure, there is a 25% margin between the acceptable maximum leakage rate and the maximum permissible leakage rate.
6.2.1.3.2 General Description of Containment Pressure Analysis The time history of conditions within an ice condenser containment during a postulated loss of coolant accident can be divided into two periods for calculation purposes:
(1) The initial reactor coolant blowdown, which for the largest assumed pipe break occurs in approximately 10 seconds.
(2) The post blowdown phase of the accident which begins following the blowdown and extends several hours after the start of the accident.
During the first few seconds of the blowdown period of the reactor coolant system, containment conditions are characterized by rapid pressure and temperature transients. It is during this period that the peak transient pressures, differential pressures, temperature and blowdown loads occur. To calculate these transients a detailed spatial and short time increment analysis was necessary. This analysis was performed with the Transient Mass Distribution (TMD) computer code (Reference 4) with the calculation time of interest extending up to a few seconds following the accident initiation (See Section 6.2.1.3.4).
Physically, tests at the ice condenser Waltz Mill test facility have shown that the blowdown phase represents that period of time in which the lower compartment air and a portion of the ice condenser air are displaced and compressed into the upper compartment and the remainder of the ice condenser. The containment pressure at or near the end of blowdown is governed by this air compression process. The containment compression ratio calculation is described in Section 6.2.1.3.4.
Containment pressure during the post blowdown phase of the accident is calculated with the LOTIC code which models the containment structural heat sinks and containment safeguards systems.
6.2.1.3.3 Long-Term Containment Pressure Analysis Early in the ice condenser development program it was recognized that there was a need for modeling of long-term ice condenser containment performance. It was realized that the model would have to have capabilities comparable to those of the dry containment (COCO) model. These capabilities would permit the model to be used to solve problems of containment design and optimize the containment and safeguards systems. This has been accomplished in the development of the LOTIC code[1].
The model of the containment consists of five distinct control volumes; the upper compartment, the lower compartment, the portion of the ice bed from which the ice has melted, the portion of the ice bed containing unmelted ice, and the dead ended compartments. The ice condenser control volume with unmelted ice is further 6.2.1-4 Containment Functional Design
WATTS BAR WBNP-112 subdivided into six subcompartments to allow for maldistribution of break flow to the ice bed.
The conditions in these compartments are obtained as a function of time by the use of fundamental equations solved through numerical techniques. These equations are solved for three distinct phases in time. Each phase corresponds to a distinct physical characteristic of the problem. Each of these phases has a unique set of simplifying assumptions based on test results from the ice condenser test facility. These phases are the blowdown period, the depressurization period, and the long term.
The most significant simplification of the problem is the assumption that the total pressure in the containment is uniform. This assumption is justified by the fact that after the initial blowdown of the reactor coolant system, the remaining mass and energy released from this system into the containment are small and very slowly changing. The resulting flow rates between the control volumes will also be relatively small. These small flow rates then are unable to maintain significant pressure differences between the compartments.
In the control volumes, which are always assumed to be saturated, steam and air are assumed to be uniformly mixed and at the control volume temperature. The air is considered a perfect gas, and the thermodynamic properties of steam are taken from the ASME steam table.
For the purpose of calculation, the condensation of steam is assumed to take place in a condensing node located between the two control volumes in the ice storage compartment.
Containment Pressure Calculation The following are the major input assumptions used in the LOTIC analysis for the pump suction pipe rupture case with the steam generators considered as an active heat source for the Watts Bar Nuclear Plant containment:
(1) Minimum safeguards are employed in all calculations, e.g., one of two spray pumps and one of two spray heat exchangers; one of two RHR pumps and one of two RHR heat exchangers providing flow to the core; one of two safety injection pumps and one of two centrifugal charging pumps; and one of two air return fans.
(2) 2.26 x 106 lbs. of ice initially in the ice condenser which is at 15°F.
(3) The blowdown, reflood, and post reflood mass and energy releases described in Section 6.2.1.3.6 were used.
(4) Blowdown and post-blowdown ice condenser drain temperatures of 190°F and 130°F are used[5].
(5) Nitrogen from the accumulators in the amount of 2955.68 lbs. included in the calculations.
Containment Functional Design 6.2.1-5
WATTS BAR WBNP-112 (6) Essential raw cooling water temperature of 88°F is used on the spray heat exchanger and the component cooling heat exchanger. Note: The containment analysis was run at an ERCW temperature of 88°F although the containment spray, component cooling, and residual heat removal heat exchanger UA values are based on an ERCW temperature of 85°F to provide additional conservatism.
(7) The air return fan is effective 10 minutes after the transient is initiated. The actual air return fan initiation can take place in 9 + 1 minutes, with initiation as early as 8 minutes not adversely affecting the analysis results.
(8) No maldistribution of steam flow to the ice bed is assumed.
(9) No ice condenser bypass is assumed. (This assumption depletes the ice in the shortest time and is thus conservative.)
(10) The initial conditions in the containment are a temperature of 120°F in the lower and dead-ended volumes, 110°F in the upper volume, and 15°F in the ice condenser. All volumes are at a pressure of 0.3 psig and a 10-percent relative humidity, except the ice condenser which is at 100-percent relative humidity.
(11) A containment spray pump flow of 4000 gpm is used in the upper compartment. The analyzed diesel loading sequence for the containment sprays to energize and come up to full flow and head in 234 seconds is tabulated in Table 6.2.1-25.
(12) A residual spray (2000 gpm design, 1475 gpm analytical) is used. The residual heat removal pump and spray pump take suction from the sump during recirculation.
During the recirculation phase of a LOCA mass and energy release transient, a portion of the RHR pump flow can be diverted to the RHR sprays. The minimum time before RHR spray can be placed in service, as indicated in the Watts Bar Nuclear Plant System Description N3-72-4001, R19, Containment Heat Removal Spray System, is at least 1 hour1.157407e-5 days <br />2.777778e-4 hours <br />1.653439e-6 weeks <br />3.805e-7 months <br /> after LOCA initiation to ensure adequate RHR flow to the core to remove the initial decay heat. Based on the preceding criteria, the RHR spray initiation was modeled at 4346.7 seconds into the LOCA containment response transient.
A discussion of the core cooling capability of the emergency core cooling system is given in Section 6.3.1 for this mode of operation.
(13) Containment structural heat sink data is found in Table 6.2.1-1. (Note: The dead-ended compartment structural heat sinks were conservatively neglected.)
6.2.1-6 Containment Functional Design
WATTS BAR WBNP-112 (14) The operation of one containment spray heat exchanger (UA = 2.44 x 106 Btu/hr-°F incorporating a 10% tube plugging margin) for containment cooling and the operation of one RHR heat exchanger (UA = 1.496 x 106 Btu/hr-°F) for core cooling. The component cooling system heat exchanger UA was modeled at 5.778 x 106 Btu/hr-°F.
(15) The air return fan returns air at a rate of 40,000 cfm from the upper to lower compartment.
(16) An active sump volume of 51,000 ft3 is used.
(17) The pump flowrates vs. time given in Table 6.2.1-2 were used in support of RWST draindown. (These flow values reflect ECCS pumps at runout against the design containment pressure, using the minimum composite pump curves shown in Figures 6.3-2, 6.3-3, and 6.3-4, which are degraded by 5%
and bound what is achievable in the plant. Switchover times from injection to recirculation that are achievable in the plant for each ECCS pump were conservatively modeled in the analysis.)
(18) A power rating of 102% of licensed core power (3411 MWt) is assumed, but not explicitly modeled. [Decay heat is based on a reactor power of 3479.22 MWt (+2%) for mass and energy release computations. See Section 6.2.1.3.6.]
(19) Hydrogen gas was added to the containment in the amount of 25,230.2 Standard Cubic Feet (SCF) over 24 hours2.777778e-4 days <br />0.00667 hours <br />3.968254e-5 weeks <br />9.132e-6 months <br />. Sources accounted for were radiolysis in the core and sump post-LOCA, corrosion of plant materials (aluminum, zinc, and painted surfaces found in containment), reaction of 1%
of the Zirconium fuel rod cladding in the core, and hydrogen gas assumed to be dissolved in the reactor coolant system water. (This bounds tritium producing core designs.)
(20) The containment compartment volumes were based on the following: upper compartment 645,818 ft3, lower compartment 221,074 ft3, and dead-ended compartment 146,600 ft3. (Note: These volumes represent TMD volumes.
For Containment Integrity Analysis, the volumes are adjusted to maximize air mass and the compression ratio.)
(21) Subcooling of emergency core cooling (ECC) water from the RHR heat exchanger is assumed.
(22) Essential raw cooling water flow to the containment spray heat exchanger was modeled as 5,200 gpm. Also, the essential raw cooling water flow to the component cooling heat exchanger was modeled as 6,250 gpm.
(23) The decay heat curve used to calculate mass and energy releases after steam generator equilibration is the same as presented in the mass and energy release section of the FSAR (subsection 6.2.1.3.6).
Containment Functional Design 6.2.1-7
WATTS BAR WBNP-112 With these assumptions, the heat removal capability of the containment is sufficient to absorb the energy releases and still keep the maximum calculated pressure well below design.
The following plots are provided:
Figure 6.2.1-1, Containment Pressure Versus Time Figure 6.2.1-2a, Upper Compartment Temperature Versus Time Figure 6.2.1-2b, Lower Compartment Temperature Versus Time Figure 6.2.1-3, Active and Inactive Sump Temperature Transients Figure 6.2.1-4, Melted Ice Mass Transient Figure 6.2.1-4a, Comparison of Containment Pressure Versus Ice Melt Tables 6.2.1-3 and 6.2.1-4 give energy accountings at various points in the transient.
As can be seen from Figure 6.2.1-1 the maximum calculated Containment pressure is 12.86 psig, occurring at approximately 4348 seconds.
Structural Heat Removal Provision is made in the containment pressure analysis for heat storage in interior and exterior walls. Each wall is divided into a number of nodes. For each node, a conservation of energy equation expressed in finite difference forms accounts for transient conduction into and out of the node and temperature rise of the node. Table 6.2.1-1 is a summary of the containment structural heat sinks used in the analysis. The material property data used is found in Table 6.2.1-5.
The heat transfer coefficient to the containment structures is based primarily on the work of Tagami, Reference [21]. An explanation of the manner of application is given in Reference [3].
When applying the Tagami correlations a conservative limit was placed on the lower compartment stagnant heat transfer coefficients. They were limited to 72 Btu/hr-ft2.
This corresponds to a steam-air ratio of 1.4 according to the Tagami correlation. The imposition of this limitation is to restrict the use of the Tagami correlation within the test range of steam-air ratios where the correlation was derived.
6.2.1.3.4 Short-Term Blowdown Analysis TMD Code - Short-Term Analysis (1) Introduction 6.2.1-8 Containment Functional Design
WATTS BAR WBNP-112 The basic performance of the ice condenser reactor containment system has been demonstrated for a wide range of conditions by the Waltz Mill Ice Condenser Test Program. These results have clearly shown the capability and reliability of the ice condenser concept to limit the Containment pressure rise subsequent to a hypothetical loss-of-coolant accident.
To supplement this experimental proof of performance, a mathematical model has been developed to simulate the ice condenser pressure transients. This model, encoded as computer program TMD (Transient Mass Distribution) Reference [4], provides a means for computing pressures, temperatures, heat transfer rates, and mass flow rates as a function of time and location throughout the containment. This model is used to compute pressure differences on various structures within the containment as well as the distribution of steam flow as the air is displaced from the lower compartment. Although the TMD code can calculate the entire blowdown transient, the peak pressure differences on various structures occur within the first few seconds of the transient.
(2) Analytical Models (No Entrainment)
The mathematical modeling in TMD is similar to that of the SATAN blowdown code in that the analytical solution is developed by considering the conservation equations of mass, momentum and energy and the equation of state, together with the control volume technique for simulating spatial variation. The governing equations for TMD are given in Reference [4].
The moisture entrainment modifications to the TMD code are discussed, in detail, in Reference [4]. These modifications comprise incorporating the additional entrainment effects into the momentum and energy equations.
As part of the review of the TMD code, additional effects are considered.
Changes to the analytical model required for these studies are described in Reference [4].
These studies consist of:
(a) Spatial acceleration effects in ice bed (b) Liquid entrainment in ice beds (c) Upper limit on sonic velocity (d) Variable ice bed loss coefficient (e) Variable door response (f) Wave propagation effects Additionally the TMD code has been modified to account for fluid compressibility effects in the high Mach number subsonic flow regime.
Containment Functional Design 6.2.1-9
WATTS BAR WBNP-112 Experimental Verification The performance of the TMD code was verified against the 1/24 scale air tests and the 1968 Waltz Mill tests. For the 1/24 scale model the TMD code was utilized to calculate flow rates to compare against experimental results. The effect of increased nodalization was also evaluated. The Waltz Mill test comparisons involved a reexamination of test data. In conducting the reanalyses, representation of the 1968 Waltz Mill test was reviewed with regard to parameters such as loss coefficients and blowdown time history. The details of this information are given in Reference [4].
The Waltz Mill Ice Condenser Blowdown Test Facility was reactivated in 1973 to verify the ice condenser performance with the following redesigned plant hardware scaled to the test configuration:
(1) Perforated metal ice baskets and new design couplings.
(2) Lattice frames sized to provide the correct loss coefficient relative to plant design.
(3) Lower support beamed structure and turning vanes sized to provide the correct turning loss relative to the plant design.
(4) No ice baskets in the lower ice condenser plenum opposite the inlet doors.
The result of these tests was to confirm that conclusions derived from previous Waltz Mill tests have not been significantly changed by the redesign of plant hardware. The TMD Code has, as a result of the 1973 test series, been modified to match ice bed heat transfer performance. Detailed information on the 1973 Waltz Mill test series is found in Reference [5].
Application to Plant Design (General Description)
As described in Reference [4], the control volume technique is used to spatially represent the containment. The containment is divided into 50 elements to give a detailed representation of the local pressure transient on the containment shell and internal concrete structures. This division of the containment is similar for all ice condenser plants.
The Watts Bar plant containment has been divided into 50 elements or compartments as shown in Figures 6.2.1-5, 6.2.1-6, 6.2.1-7, and 6.2.1-8. The interconnections between containment elements in the TMD code is shown schematically in Figure 6.2.1-9. Flow resistance and inertia are lumped together in the flow paths connecting the elements shown. The division of the lower compartments into 6 volumes occurs at the points of greatest flow resistance, i.e., the four steam generators, pressurizer and refueling cavity.
Each of these lower compartment sections delivers flow through doors into a section behind the doors and below the ice bed. Each vertical section of the ice bed is, in turn, divided into three elements. The upper plenum between the top of the ice bed and the upper doors is represented by an element. Thus, a total of thirty elements (Elements 6.2.1-10 Containment Functional Design
WATTS BAR WBNP-112 7 through 24 and 38 through 49 are used to simulate the ice condenser). The six elements at the top of the ice bed between bed and upper doors deliver to element number 25 the upper compartment. Note that cross flow in the ice bed is not accounted for in the analysis; this yields the most conservative results for the particular calculations described herein. The upper reactor cavity (Element 33) is connected to the lower compartment volumes and provides cross flow for pressure equalization of the lower compartments. The less active compartments, called dead-ended compartments (Elements 26 through 32 and 34 through 37) outside the crane wall are pressurized by ventilation openings through the crane wall into the fan compartments.
For each element in the TMD network the volume, initial pressure and initial temperature conditions are specified. The ice condenser elements have additional inputs of mass of ice, heat transfer area and condensate layer length. For each flow path between elements flow resistance is specified as a loss coefficient "K" or a fraction loss "L/D" or a combination of the two based on the flow area specified between elements. Friction factor, friction factor length and hydraulic diameter are specified for the friction loss.
Additionally, input for each flow path includes the area ratio (minimum area/maximum area) which is used to account for compressibility effects across flow path contractions.
The code input for each flow path is the flow path length used in the momentum equation. The ice condenser loss coefficients have been based on the 1/4-scale tests representative of the current ice condenser geometry. The test loss coefficient was increased to include basket roughness effects and to include intermediate and top deck pressure losses. The loss coefficient is based on removal of door port flow restrictors.
To better represent short term transients effects, the opening characteristics of the lower, intermediate, and top deck ice condenser doors have been modeled in the TMD code. The containment geometric data for the elements and flow paths used in the TMD code is confirmed to agree with the actual design by TVA and Westinghouse. An initial containment pressure of 0.3 psig was assumed in the analysis. Initial containment pressure variation about the assumed 0.3 psig value has only a slight affect on the initial pressure peak and the compression ratio pressure peak. TMD input data is given in Tables 6.2.1-6 and 6.2.1-7.
The reactor coolant blowdown rates used in these cases are based on the SATAN analysis of a double-ended rupture of either a hot or a cold leg reactor coolant pipe utilizing a discharge coefficient of 1.0. The models and assumptions used to calculate the short-term mass and energy releases are described in Reference [9]. Tables 6.2.1-23 and 6.2.1-24 present the mass and energy release data used for this analysis.
A number of analyses have been performed to determine the various pressure transients resulting from hot and cold leg reactor coolant pipe breaks in any one of the six lower compartment elements. The analyses were performed using the following assumptions and correlations:
(1) Flow was limited by the unaugmented critical flow correlation.
Containment Functional Design 6.2.1-11
WATTS BAR WBNP-112 (2) The TMD variable volume door model, which accounts for changes in the volumes of TMD elements as the door opens, was implemented.
(3) The heat transfer calculation used was based on performance during the 1973-1974 Waltz Mill test series. A higher value of the ELJAC parameter has been used and an upper bound on calculated heat transfer coefficients has been imposed[5].
(4) One hundred percent moisture entrainment was assumed.
(5) Compressibility effects due to flow area contractions were modeled.
Figures 6.2.1-10 and 6.2.1-11 are representative of the typical upper and lower compartment pressure transients that result from a hypothetical double-ended rupture of a reactor coolant pipe for the worst possible location in the lower compartment of the containment; i.e., hot leg and cold leg breaks in Element 1.
Initial Pressures Results of the analysis for the Watts Bar Plant are presented in Tables 6.2.1-8 through 6.2.1-11. The peak pressures and peak differential pressures resulting from hot and cold leg reactor coolant pipe breaks in each of the six lower compartment control volumes were calculated.
Table 6.2.1-8 presents the maximum calculated pressure peak for the lower compartment elements resulting from hot and cold leg double ended pipe breaks.
Generally, the maximum peak pressure within a lower compartment element results when the pipe break occurs in that element. A cold leg break in Element 1 creates the highest pressure peak, also in Element 1, of 18.5 psig.
Table 6.2.1-9 presents the maximum calculated peak pressure in each of the ice condenser sections resulting from any pipe break location. The maximum peak pressure in each of the ice condenser sections is found in the lower plenum element of the section. The peak pressure was calculated to be 13.9 psig in Element 40.
Table 6.2.1-10 presents the maximum calculated differential pressures across the operating deck (divider barrier) between the lower compartment elements and the upper compartment. These values are approximately the same as the maximum calculated differential pressure across the lower crane wall between the lower compartment elements and the dead ended volumes surrounding the lower compartment. The peak differential pressure of 16.6 psi was calculated to be between Elements 1 and 25 for a cold leg break.
Table 6.2.1-11 presents the maximum calculated differential pressures across the upper crane wall between the upper ice condenser elements and the upper compartment. The peak differential of 8.4 psi pressure was calculated to be between Element 7-8-9 and 25 for a hot leg pipe break.
6.2.1-12 Containment Functional Design
WATTS BAR WBNP-112 Consideration is given to the calculation of subcompartment pressures (and pressure differentials) for cases other than the design basis double ended reactor coolant pipe rupture in the lower compartment. Discussion of these analyses is treated in Section 6.2.1.3.9.
Sensitivity Studies A series of TMD runs for D. C. Cook investigated the sensitivity of peak pressures to variations in individual input parameters for the design basis blowdown rate and 100 percent entrainment. This analysis used a DEHL break in Element 6 of D. C. Cook.
Table 6.2.1-12 presents the results of this sensitivity study.
As part of the short-term containment pressure analysis of ice condenser units, the pressure response to both DEHL and DECL breaks are routinely considered for each of the loop compartments.
Choked Flow Characteristics The data in Figure 6.2.1-12 illustrate the behavior of mass flow rate as a function of upstream and downstream pressures, including the effects of flow choking. The upper plot shows mass flow rate as a function of upstream pressure for various assumed values of downstream pressure. For zero back pressure (Pd = 0), the entire curve represents choked flow conditions with the flow rate approximately proportional to upstream pressure Pu. For higher back pressure, the flow rates are lower until the upstream pressure is high enough to provide choked flow. After the increase in upstream pressure is sufficient to provide flow chokings further increases in upstream pressure cause increases in mass flow rate along the curve for Pd = 0. The key point in this illustration is that flow rate continues to increase with increasing upstream pressure, even after flow choking conditions have been reached. Thus, choking does not represent a threshold beyond which dramatically sharper increases in compartment pressures could be expected because of limitations on flow relief to adjacent compartments.
The phenomenon of flow choking is more frequently explained by assuming a fixed upstream pressure and examining the dependence of flow rate with respect to decreasing downstream pressure. This approach is illustrated for an assumed upstream pressure of 30 psia as shown in the upper plot with the results plotted vs.
downstream pressure in the lower plot. For fixed upstream conditions, flow choking represents an upper limit flow rate beyond which further decreases in back pressure do not produce any increase in mass flow rate.
Compression Ratio Analysis As blowdown continues following the initial pressure peak from a double-ended cold leg break, the pressure in the lower compartment again increases, reaching a peak at or before the end of blowdown. The pressure in the upper compartment continues to rise from beginning of blowdown and reaches a peak which is approximately equal to the lower compartment pressure. After blowdown is complete, the steam in the lower Containment Functional Design 6.2.1-13
WATTS BAR WBNP-112 compartment continues to flow through the doors into the ice bed compartment and is condensed.
The primary factor in producing this upper containment pressure peak and, therefore, in determining design pressure, is the displacement of air from the lower compartment into the upper containment. The ice condenser quite effectively performs its function of condensing virtually all the steam that enters the ice beds. Essentially, the only source of steam entering the upper containment is from leakage through the drain holes and other leakage around crack openings in hatches in the operating deck separating the lower and upper portions of the containment building.
A method of analysis of the compression peak pressure was developed based on the results of full-scale section tests. This method consists of the calculation of the air mass compression ratio, the polytropic exponent for the compression process, and the effect of steam bypass through the operating deck on this compression.
The compression peak pressure in the upper containment for the Watts Bar plant design is calculated to be 7.81 psig (for an initial air pressure of 0.3 psig). This compression pressure includes the effect of a pressure increase of 0.4 psi from steam bypass and also for the effects of the dead-ended volumes. The nitrogen partial pressure from the accumulators is not included since this nitrogen is not added to the containment until after the compression peak pressure has been reduced, which is after blowdown is completed. This nitrogen is considered in the analysis of pressure decay following blowdown as presented in the long term performance analysis using the LOTIC code. The following sections discuss the major parameters affecting the compression peak. Specifically they are: air compression, steam bypass, blowdown rate, and blowdown energy.
Air Compression Process Description The volumes of the various containment compartments determine directly the air volume compression ratio. This is basically the ratio of the total active containment air volume to the compressed air volume during blowdown. During blowdown air is displaced from the lower compartment and compressed into the ice condenser beds and into the upper containment above the operating deck. It is this air compression process which primarily determines the peak in containment pressure, following the initial blowdown release. A peak compression pressure of 7.81 psig is based on the Watts Bar Plant design compartment volumes shown in Table 6.2.1-13.
Figure 6.2.1-13 shows the sensitivity of the compression peak pressure with different air compression ratios.
Methods of Calculation and Results Full-Scale Section Tests The actual Waltz Mill test compression ratios were found by performing air mass balances before the blowdown and at the time of the compression peak pressure, 6.2.1-14 Containment Functional Design
WATTS BAR WBNP-112 using the results of three full-scale special section tests. These three tests were conducted with an energy input representative of the plant design.
In the calculation of the mass balance for the ice condenser, the compartment is divided into two sub-volumes; one volume representing the flow channels and one volume representing the ice baskets. The flow channel volume is further divided into four sub-volumes. The partial air pressure and mass in each sub-volume is found from thermocouple readings by assuming that the air is saturated with steam at the measured temperature. From these results, the average temperature of the air in the ice condenser compartment is found, and the volume occupied by the air at the total condenser pressure is found from the equation of state as follows:
M a2 R a T a2 V a2 = ---------------------------- (1)
P2 where:
Va2 = Volume of ice condenser occupied by air (ft3)
Ma2 = Mass of air in ice condenser compartment (lb)
Ta2 = Average temperature of air in ice condenser (°F)
P2 = Total ice condenser pressure (lb/ft2)
Ra = Ideal gas constant The partial pressure and mass of air in the lower compartment are found by averaging the temperatures indicated by the thermocouples located in that compartment and assuming saturation conditions. For these three tests, it was found that the partial pressure, and hence the mass of air in the lower compartment, was zero at the time of the compression peak pressure.
The actual Waltz Mill test compression ratio is then found from the following:
V1 + V2 + V3 C = -------------------------------- (2)
V 3 + V a2 where:
V1 = Lower compartment volume (ft3)
V2 = Ice condenser compartment volume (ft3)
Containment Functional Design 6.2.1-15
WATTS BAR WBNP-112 V3 = Upper compartment volume (ft3)
The polytropic exponent for these tests is then found from the measured compression pressure and the compression ratio calculated above. Also considered is the pressure increase that results from the leakage of steam through the deck into the upper compartment.
The compression peak pressure in the upper compartment for the tests or containment design is then given by:
n P = P o (Cr ) + Pdeck (3) where:
Po = Initial pressure (psia)
P = Compression peak pressure (psia)
Cr = Volume compression ratio n = Polytropic exponent Pdeck = Pressure increase caused by deck leakage (psi)
Using the method of calculation described above, the compression ratio is calculated for the three full-scale section tests. From the results of the air mass balances, it was found that air occupied 0.645 of the ice condenser compartment volume at the time of peak compression, or V a2 = 0.645 V 2 (4)
The final compression volume includes the volume of the upper compartment as well as part of the volume of air in the ice condenser. The results of the full-scale section tests (Figure 6.2.1-14) show a variation in steam partial pressure from 100% near the bottom of the ice condenser to essentially zero near the top. The thermocouples and pressure detectors confirm that at the time when the compression peak pressure is reached steam occupies less than half of the volume of the ice condenser. The analytical model used in defining the containment pressure peak uses upper compartment volume plus 64.5% of the ice condenser air volumes as the final volume.
This 64.5% value was determined from appropriate test results.
The calculated volume compression ratios are shown in Figure 6.2.1-15, along with the compression peak pressures for these tests. The compression peak pressure is determined from the measured pressure, after accounting for the deck leakage contribution. From the results shown in Figure 6.2.1-15, the polytropic exponent for these tests is found to be 1.13.
6.2.1-16 Containment Functional Design
WATTS BAR WBNP-112 Plant Case For the Watts Bar design, the volume compression ratio is calculated using Equation 2, modeling the upper plenum as part of the upper compartment, and Table 6.2.1-13 as:
1, 077, 012 C r = --------------------------------------------------------------------------------- (5) 692, 818 + [ 0.645 X 110, 520 ]
Cr = 1.4095 The peak compression pressure, based on an initial containment pressure of 15.0 psia (0.3 psig), is then given by Equation 3 as:
P3 = 15.0 (1.4095)1.13 + 0.4 P3 = 22.507 psia or 7.81 psig This peak compression pressure includes a pressure increase of 0.4 psi from steam bypass through the deck (see Section 6.2.1.3.5).
Sensitivity to Blowdown Energy The sensitivity of the upper and lower compartment peak pressure versus blowdown rate as measured from the 1974 Waltz Mill Tests is shown in Figure 6.2.1-16. This figure shows the magnitude of the peak pressure versus the amount of energy released in terms of percentage of RCS energy release rate.
Percent energy blowdown rate was selected for the plot because energy flow rate more directly relates to volume flow rate and therefore pressure. There are two important effects to note from the peak upper compartment pressure versus blowdown rate:
(1) the magnitude of the final peak pressure in the upper compartment is low (about 9 psig) for the plant design DECL blowdown rate; (2) even an increase in this rate up to 141% of the blowdown energy rate produces only a small increase in the magnitude of this peak pressure (about 1 psi). The major factor setting the peak pressure reached in the upper compartment is the compression of air displaced by steam from the lower compartment into the upper compartment. The lower compartment initial peak pressure shows a relatively low peak pressure of 12.9 psig for the design basis DECL blowdown rate, and even a substantial increase in blowdown energy rate (141%
reference initial DECL) would cause an increase in initial peak pressure of only 3 psi.
The peak pressure in the lower compartment is due mainly to flow resistance caused by displacement of air from the lower compartment into the upper compartment.
6.2.1.3.5 Effect of Steam Bypass The sensitivity of the compression peak pressure to deck bypass is shown in Figure 6.2.1-17, which shows that an increase in deck bypass area of 50% would cause an increase of about 0.2 psi in final peak compression pressure. Also, it is important to note that the plant final peak compression pressure of 7.81 psig already includes a contribution of 0.4 psi from the plant deck bypass area of 5 ft2.
Containment Functional Design 6.2.1-17
WATTS BAR WBNP-112 This effect of deck leakage on upper containment pressure has been verified by a series of four special, full-scale section tests. These tests were all identical except different size deck leakage areas were used.
The results of these tests are given in Figure 6.2.1-18 which includes two curves of test results. Each curve shows the difference in upper compartment pressure between one test and another resulting from a difference in deck leakage area. One curve shows the increase in upper compartment pressure at the end of the boiler blowdown (after the compression peak pressure, at about 50 seconds in these tests), and the second curve shows the increase in upper compartment peak pressure (at about 10 seconds in these tests). It should be noted that the pressure at the end of the blowdown is less than the peak compression ratio pressure occurring at about 10 seconds for reference blowdown test.
The containment pressure increase due to deck leakage is directly proportional to the total amount of steam leakage into the upper compartment, and the amount of this steam leakage is, in turn, proportional to the amount of steam released from the boiler, less the inventory of steam remaining in the lower compartment. Notably, the increase in upper compartment compression peak pressure is substantially less than the upper compartment pressure increase at the end of blowdown, because the peak compression pressure occurs before the boiler has released all of its energy.
The calculated maximum pressure rise due to deck leakage (when all of the boiler energy release has occurred) is also shown in Figure 6.2.1-18. The slope of this curve is 0.095 psi/ft2 for the tests and is equivalent to 0.107 psi/ft2 for the plant design. The difference between the two coefficients is due to a small difference in upper compartment volume between the plant design and these tests.
As shown in Figure 6.2.1-18, the calculated curve for maximum pressure increase at the end of blowdown agrees closely with the measured curve at small deck leakage areas but deviates at larger leakage areas. This deviation apparently results from the condensation of upper compartment steam by the walls of the upper compartment and by the ice at the top of the condenser during the tests. Pressure would also be reduced by heat losses in a plant; however, for conservatism, no credit is taken for this effect.
As demonstrated by tests, the compression peak pressure in the upper compartment occurs before the boiler releases all of its energy, and the measured increase in peak compression pressure due to increased deck leakage, is proportionately reduced. For the case of the plant design, the final peak compression pressure is conservatively assumed to occur when the reactor coolant system release is 75% of its total energy.
This value is selected as a reference value, based on the results of a number of tests conducted with different blowdown rates and total energy releases, as shown in Figure 6.2.1-19. The actual deck leakage coefficient is therefore:
P 3
- = 0.107 x 0.75 = 0.080psi/ft 2 A deck 6.2.1-18 Containment Functional Design
WATTS BAR WBNP-112 The divider barrier including the enclosures over the pressurizer, steam generators and reactor vessel, is designed to provide a reasonably tight seal against leakage.
Holes are purposely provided in the bottom of the refueling cavity to allow water from sprays in the upper compartment to drain to the sump in the lower compartment.
Potential leakage paths exist at all the joints between the operating deck and the pump access hatches and reactor vessel enclosure slabs. The total of all deck leakage flow areas is approximately 5 ft2. The effect of this potential leakage path is small and is found to be:
Pdeck = 5 x 0.080 = 0.4 psi In the event that the reactor coolant system break flow is so small that it would leak through these flow paths without developing sufficient differential pressure (1 lb/ft2) to open the ice condenser doors, steam from the break would slowly pressurize the containment. The containment spray system has sufficient capacity to maintain pressure well below design for this case.
The Watts Bar Nuclear Plant and the Sequoyah Nuclear Plant are geometrically very similar. Some differences between the two plants, are the design pressure, spray flow rates, and a slight difference in thermal ratings. The fact that the spray flow rate is higher for the Sequoyah plant (4750 gpm versus 4000 gpm) is offset by Watts Bar's higher maximum internal pressure (15 psig versus 12 psig). The following discussion presents the deck leakage analysis performed for the Sequoyah plant. The purpose of this analysis is only to show the substantial margin which exists between the design deck leakage of 5 ft2 and the tolerable deck leakage. The Sequoyah analysis which shows conservatism by a factor of 7, is more than sufficient for this purpose.
The method of analysis used to obtain the maximum allowable deck leakage capacity as a function of the primary system break size is as follows.
During the blowdown transient, steam and air flow through the ice condenser doors and also through the deck bypass area into the upper compartment. For the containment, this bypass area is composed of two parts, a known leakage area of 2.2 ft2 with a geometric loss coefficient of 1.5 through the deck drainage holes location at the bottom of the refueling canal and an undefined deck leakage area with a conservatively small loss coefficient of 2.5.
A resistance network similar to that used to TMD is used to represent 6 lower compartment volumes each with a representative portion of the deck leakage, and the lower inlet door flow resistance and flow area is calculated for small breaks that would only partially open these doors. The coolant blowdown rate as a function of time is used with this flow network to calculate the differential pressures on the lower inlet doors and across the operating deck.
The resultant deck leakage rate and integrated steam leakage into the upper compartment is then calculated. The lower inlet doors are initially held shut by the cold head of air behind the doors (approximately one pound per square foot). The initial blowdown from a small break opens the doors and removes the cold head on the doors. With the door differential removed, the door position is slightly open. An Containment Functional Design 6.2.1-19
WATTS BAR WBNP-112 additional pressure differential of one pound per square foot is then sufficient to fully open the doors. The nominal door opening characteristics are based on test results.
One analysis conservatively assumed that flow through the postulated leakage paths is pure steam. During the actual blowdown transient, steam and air representative of the lower compartment mixture leak through the holes, thus less steam would enter the upper compartment. If flow were considered to be a mixture of liquid and vapor, the total leakage mass would increase, but the steam flow rate would decrease. The analysis also assumed that no condensing of the flow occurs due to structural heat sinks. The peak air compression in the upper compartment for the various break sizes is assumed with steam mass added to this value to obtain the total containment pressure. Air compression for the various break sizes is obtained from previous full-scale section tests conducted at Waltz Mill.
The allowable leakage area for the following reactor coolant system (RCS) break sizes was determined: DE, 0.6 DE, 3 ft2, 10 inch diameter, 6 inch diameter, 2 inch diameter, and 0.5 inch diameter. The allowable deck leakage area for the DE break was based on the test results previously discussed. For break sizes of 3 ft2 and 0.6 DE, a series of deck leakage sensitivity studies were made to establish the total steam leakage to the upper compartment over the blowdown transient. This steam was added to the peak compression air mass in the upper compartment to calculate a peak pressure.
Air and steam were assumed to be in thermal equilibrium, with the air partial pressure increased over the air compression value to account for heating effects. For these breaks, sprays were neglected. Reduction in compression ratio by return of air to the lower compartment was conservatively neglected. The results of this analysis are shown in Table 6.2.1-14. This analysis is confirmed by Waltz Mill tests conducted with various deck leaks equivalent to over 50 ft2 feet of deck leakage for the double-ended blowdown rate and is shown in Figure 6.2.1-20.
For breaks of 10 inch diameter and smaller, the effect of containment sprays was included. The method used calculates, for each time step of the blowdown, the amount of steam leaking into the upper compartment to obtain the steam mass in the upper compartment. This steam was mixed with the air in the upper compartment, assuming thermal equilibrium with air. The air partial pressure was increased to account for air heating effects. After sprays were initiated, the pressure was calculated based on the rate of accumulation of steam in the upper compartment.
This analysis was conducted for the 10 inch, 6 inch, and 2 inch break sizes, assuming one spray pump operated (4750 gpm at 100°F). As shown in Table 6.2.1-14, the 10 inch break is the limiting case for the given range of break sizes.
A second, more realistic, method was used to analyze the 10 inch, 6 inch, and 2 inch breaks. This analysis assumed a 30% air and 70% steam mix flowing through the deck leakage area. This is conservative considering the amount of air in the lower compartment during this portion of the transient. Operation of the deck fan increases the air content of the lower compartment, thus increasing the allowable deck leakage area. Based on the LOTIC code analysis, a structural heat removal rate of over 6000 Btu/sec from the upper compartment is indicated. Therefore, a steam condensation 6.2.1-20 Containment Functional Design
WATTS BAR WBNP-112 rate of 6 lbs/sec was used for the upper compartment. The results indicate that with one spray pump operating and a deck leakage area of 50 ft2, the peak containment pressure is below design pressure.
The 1/2 inch diameter break is not sufficient to open the ice condenser inlet doors. For this break, the upper compartment spray is sufficient to condense the break steam flow.
In conclusion, it is apparent that there is a substantial margin between the design deck leakage area of 5 ft2 and that which can be tolerated without exceeding containment design pressure. A preoperational visual inspection is performed to ensure that the seals between the upper and lower containment have been properly installed.
6.2.1.3.6 Mass and Energy Release Data Long-Term Loss-of-Coolant Accident Mass and Energy Releases The evaluation model used for the long-term LOCA mass and energy release calculations is the March 1979 model described in Reference 20. This evaluation model has been reviewed and approved by the NRC.
The time history of conditions within an ice condenser containment during a postulated loss-of-coolant accident (LOCA) can be divided into two periods:
- 1. The initial reactor coolant blowdown, which for the largest assumed pipe break occurs within approximately 30 seconds.
- 2. The post blowdown phase of the accident which begins following the blowdown and extends several hours after the start of the accident.
LOCA Mass and Energy Release Phases The containment system receives mass and energy releases following a postulated rupture in the RCS. These releases continue over a time period, the LOCA analysis calculational model is typically divided into four phases:
- 1. Blowdown - the period of time from accident initiation (when the reactor is at steady-state operation) to the time that the RCS and containment reach an equilibrium state at containment design pressure.
- 2. Refill - the period of time when the reactor vessel lower plenum is being filled by accumulator and Emergency Core Cooling System (ECCS) water. At the end of blowdown, a large amount of water remains in the cold legs, downcomer, and lower plenum. To conservatively consider the refill period for the purpose of containment mass and energy releases, it is assumed that this water is instantaneously transferred to the lower plenum along with sufficient accumulator water to completely fill the lower plenum. This allows an uninterrupted release of mass and energy to containment. Therefore, the refill period is conservatively neglected in the mass and energy release calculation.
Containment Functional Design 6.2.1-21
WATTS BAR WBNP-112
- 3. Reflood - begins when the water from the reactor vessel lower plenum enters the core and ends when the core is completely quenched.
- 4. Post-reflood (Froth) - describes the period following the reflood transient. For the pump suction break, a two-phase mixture exits the core, passes through the hot legs, and is superheated in the steam generators prior to release to containment.
After the broken loop steam generator cools, the break flow becomes two phase.
Break Size and Location Generic studies have been performed with respect to the effect of postulated break size on the LOCA mass and energy releases. The double-ended guillotine break has been found to be limiting due to larger mass flow rates during the blowdown phase of the transient. During the reflood and froth phases, the break size has little effect on the releases.
Three distinct locations in the RCS loop can be postulated for pipe rupture:
- 1. Hot leg (between vessel and steam generator)
- 2. Cold leg (between pump and vessel)
- 3. Pump suction (between steam generator and pump)
For long-term considerations the break location analyzed is the pump suction double-ended guillotine (DEPSG) (10.46 ft2). The pump suction break mass and energy releases have been calculated for the blowdown, reflood, and post-reflood phases of the LOCA for each case analyzed. The following paragraphs provide a discussion on each break location.
The hot-leg double-ended guillotine has been shown in previous studies to result in the highest blowdown mass and energy release rates. Although the core flooding rate would be the highest for this break location, the amount of energy released from the steam generator secondary is minimal because the majority of the fluid that exits the core bypasses the steam generators, venting directly to containment. As a result, the reflood mass and energy releases are reduced significantly as compared to either the pump suction or cold-leg break locations, where the core exit mixture must pass through the steam generators before venting through the break.
For the hot-leg break, generic studies have confirmed that there is no reflood peak (that is, from the end of the blowdown period the containment pressure would continually decrease). The mass and energy releases for the hot-leg break have not been included in the scope of this containment integrity analysis because, for the hot-leg break, only the blowdown phase of the transient is of any signifcance. Since there are no reflood or post-reflood phases to consider, the limiting peak pressure calculated would be the compression peak pressure and not the peak pressure following ice bed melt-out.
The cold-leg break location has been found in previous studies to be much less limiting in terms of the overall containment energy releases. The cold-leg blowdown is faster 6.2.1-22 Containment Functional Design
WATTS BAR WBNP-112 than that of the pump suction break, and more mass is released into the containment.
However, the core heat transfer is greatly reduced, and this results in a considerably lower energy release into containment. Studies have determined that the blowdown transient for the cold leg is less limiting than that tor the pump suction break. During cold-leg reflood, the flooding rate is greatly reduced and the energy release rate into the containment is reduced. Therefore, the cold-leg break is not included in the scope of this analysis.
The pump suction break combines the effects of the relatively high core flooding rate, as in the hot-leg break, and the addition of the stored energy in the steam generators.
As a result, the pump suction break yields the highest energy flow rates during the post-blowdown period by including all of the available energy of the RCS in calculating the releases to containment. This break has been determined to be the limiting break for all ice condenser plants.
In summary, the analysis of the limiting break location for an ice condenser containment has been performed. The DEPSG break has historically been considered to be the limiting break location, by virtue of its consideration of alI energy sources in the RCS. This break location provides a mechanism for the release of the available energy in the RCS, including both the broken and intact loop steam generators.
Inclusion of these energy sources conservatively results in the maximum amount of ice being melted in the event of a LOCA.
Application of Single-Failure Criteria An analysis of the effects of the single-failure criteria has been performed on the mass and energy release rates for the pump suction (DEPSG) break. An inherent assumption in the generation of the mass and energy release is that offsite power is lost. This results in the actuation of the emergency diesel generators, required to power the Safety Injection System. This is not an issue for the blowdown period, which is limited by the compression peak pressure.
The limiting minimum safety injection case has been analyzed for the effects of a single failure. In the case of minimum safeguards, the single failure postulated to occur is the loss of an emergency diesel generator. This results in the loss of one pumped safety injection train, that is, ECCS pumps and heat exchangers.
Basis of the Analysis I. Significant Modeling Assumptions The following summarized assumptions were employed to ensure that the mass and energy releases were conservatively calculated, thereby maximizing energy release to containment:
- 1. Maximum expected operating temperature of the RCS at 100-percent full-power conditions: (619.1°F)
Containment Functional Design 6.2.1-23
WATTS BAR WBNP-112
- 2. An alIowance in temperature for instrument error and dead band was assumed on the vessel/core inlet temperature (+7.0°F)
- 3. Margin in volume of 3 percent (which is composed of a 1.6-percent allowance for thermal expansion, and a 1.4-percent alIowance for uncertainty)
- 4. Core rated power of 3,411 MWt
- 5. Allowance for calorimetric error (+2.0 percent of power)
- 6. Conservative coefficient of heat transfer (that is, steam generator primary/secondary heat transfer and RCS metal heat transfer).
- 7. Core-stored energy based on the time in life for maximum fuel densification. The assumptions used to calculate the fuel temperatures for the core-stored energy calculation account for appropriate uncertainties associated with the models in the PAD code (such as calibration of the thermal model, pellet densification model, or clad creep model). In addition, the fuel temperatures for the core-stored energy calculation account for appropriate uncertainties associated with manufacturing tolerances (such as pellet as-built density). The total uncertainty for the fuel temperature calculation is a statistical combination of these effects and is dependent upon fuel type, power level, and burnup.
- 8. An allowance for RCS initial pressure uncertainty (+70 psi)
- 9. A maximum containment backpressure equal to design pressure
- 10. A provision for modeling steam flow in the secondary side through the steam generator turbine stop valve was conservatively addressed only at the start of the event. A turbine stop valve isolation time equal to 0.0 seconds was used.
- 11. As noted in Section 2.4 of Reference 20, the option to provide more specific modeling pertaining to decay heat has been exercised to specifically reflect the Watts Bar Nuclear Plant Unit 2 core heat generation, while retaining the two sigma uncertainty to assure conservatism.
- 12. Steam generator tube plugging leveling (0-percent uniform)
- a. Maximizes reactor coolant volume and fluid release
- b. Maximizes heat transfer area across the steam generators tubes
- c. Reduces coolant loop resistance, which reduces the p upstream of the break and increases break flow 6.2.1-24 Containment Functional Design
WATTS BAR WBNP-112 II. Initial Conditions Table 6.2.1-15 presents the System Parameters Initial Conditions utilized.
Thus, based on the previously noted conditions and assumptions, a bounding analysis of Watts Bar Nuclear Plant Unit 2 is made for the release of mass and energy from the RCS in the event of a LOCA.
Blowdown Mass and Energy Release Data A version of the SATAN-VI code is used for computing the blowdown transient, which is the code used for the ECCS calculation in Reference 22. The SATAN-VI code calculates blowdown (the first portion of the thermal-hydraulic transient following break initiation), including pressure, enthalpy, density, mass, energy flow rates, and energy transfer between primary and secondary systems as a function of time.
The code utilizes the control volume (element) approach with the capability for modeling a large variety of thermal fluid system configurations. The fluid properties are considered uniform and thermodynamic equilibrium is assumed in each element. A point kinetics model is used with weighted feedback effects. The major feedback effects include moderator density, moderator temperature, and Doppler broadening. A critical flow calculation for subcooled (modified Zaloudek), two-phase (Moody), or superheated break flow is incorporated into the analysis. The methodology for the use of this model is described in Reference 20.
Table 6.2.1-16 presents the calculated LOCA mass and energy releases for the blowdown phase of the DEPSG break. For the pump suction breaks, break path 1 in the mass and energy release tables refers to the mass and energy exiting from the steam generator side of the break; break path 2 refers to the mass and energy exiting from the pump side of the break.
Reflood Mass and Energy Release Data The WREFLOOD code used for computing the reflood transient is a modified version of that used in the 1981 ECCS evaluation model, Reference 22. The WREFLOOD code addresses the portion of the LOCA transient where the core reflooding phase occurs after the primary coolant system has depressurized (blowdown) due to the loss of water through the break and when water supplied by the emergency core cooling refills the reactor vessel and provides cooling to the core. The most important feature is the steam/water mixing model.
The WREFLOOD code consists of two basic hydraulic models - one for the contents of the reactor vessel and one for the coolant loops. The two models are coupled through the interchange of the boundary conditions applied at the vessel outlet nozzles and at the top of the downcomer. Additional transient phenomena, such as pumped safety injection and accumulators, reactor coolant pump performance, and steam generator release are included as auxiliary equations that interact with the basic models as required. The WREFLOOD code permits the capability to calculate variations (during the core reflooding transient) of basic parameters such as core Containment Functional Design 6.2.1-25
WATTS BAR WBNP-112 flooding rate, core and downcomer water levels, fluid thermodynamic conditions (pressure, enthalpy, density) throughout the primary system, and mass flow rates through the primary system. The code permits hydraulic modeling of the two flow paths available for discharging steam and entrained water from the core to the break; that is, the path through the broken loop and the path through the unbroken loops.
A complete thermal equilibrium mixing condition for the steam and emergency core cooling injection water during the reflood phase has been assumed for each loop receiving ECCS water. This is consistent with the usage and application of the Reference 4 mass and energy release evaluation model. Even though the Reference 20 model credits steam/mixing only in the intact loop and not in the broken loop, justification, applicability, and NRC approval for using the mixing model in the broken loop has been documented (Reference 23). This assumption is justified and supported by test data, and is summarized as follows.
The model assumes a complete mixing condition (that is, thermal equilibrium) for the steam/water interaction. The complete mixing process is made up of two distinct physical processes. The first is a two-phase interaction with condensation of steam by cold ECCS water. The second is a single-phase mixing of condensate and ECCS water. Since the steam release is the most important influence to the containment pressure transient, the steam condensation part of the mixing process is the only part that need be considered. (Any spillage directly heats only the sump.)
The most applicable steam/water mixing test data has been reviewed for validation of the containment integrity reflood steam/water mixing model. This data is generated in 1/3 scale tests (Reference 24), which are the largest scale data available and thus most clearly simulate the flow regimes and gravitational effects that would occur in a pressurized water reactor (PWR). These tests were designed specifcally to study the steam/water interaction for PWR reflood conditions.
From the entire series of 1/3 scale tests, one group corresponds almost directly to containment integrity reflood conditions. The injection flow rates from this group cover all phases and mixing conditions calculated during the reflood transient. The data from these tests were reviewed and discussed in detail in Reference 20. For all of these tests, the data clearly indicate the occurrence of very effective mixing with rapid steam condensation. The mixing model used in the containment integrity reflood calculation is therefore wholly supported by the 1/3 scale steam/water mixing data.
Additionally, the following justification is also noted. The post-blowdown limiting break for the containment integrity peak pressure analysis is the DEPSG break. For this break, there are two flow paths available in the RCS by which mass and energy may be released to containment. One is through the outlet of the steam generator, the other is via reverse flow through the reactor coolant pump. Steam that is not condensed by ECCS injection in the intact RCS loops passes around the downcomer and through the broken loop cold leg and pump in venting to containment. This steam also encounters ECCS injection water as it passes through the broken loop cold leg, complete mixing occurs and a portion of it is condensed. It is this portion of steam, which is condensed, for which this analysis takes credit. This assumption is justified based upon the 6.2.1-26 Containment Functional Design
WATTS BAR WBNP-112 postulated break location and the actual physical presence of the ECCS injection nozzle. A description of the test and test results is contained in References 20 and 24.
Table 6.2.1-17 presents the calculated mass and energy release for the reflood phase of the pump suction double ended rupture with minimum safety injection.
The transients of the principal parameters during reflood are given in Table 6.2.1-18.
Post-Reflood Mass and Energy Release Data The FROTH code (Reference 9) is used for computing the post-reflood transient. The FROTH code is used for the steam generator heat addition calculation from the broken and intact loop steam generators.
The FROTH code calculates the heat release rates resulting from a two-phase mixture level present in the steam generator tubes. The mass and energy releases that occur during this phase are typically superheated due to the depressurization and equilibration of the broken loop and intact loop steam generators. During this phase of the transient, the RCS has equilibrated with the containment pressure, but the steam generators contain a secondary inventory at an enthalpy that is much higher than the primary side. Therefore, a significant amount of reverse heat transfer occurs. Steam is produced in the core due to core decay heat. For a pump suction break, a two-phase fluid exits the core, flows through the hot legs, and becomes superheated as it passes through the steam generator. Once the broken loop cools, the break flow becomes two-phase. The methodology for the use of this model is described in Reference 20.
The EPITOME code continues the FROTH post-reflood portion of the transient from the time at which the secondary side equilibrates to containment design pressure to the end of the transient. It also compiles a summary of data on the entire transient, including formal instantaneous mass and energy release tables and mass and energy balance tables with data at critical times.
After steam generator depressurization/equilibration, the mass and energy release available to containment is generated directly from core boiloff/decay heat. At this time the flow split is assumed to be 100%.
Table 6.2.1-19 presents the two-phase post-reflood (froth) mass and energy release data for the pump suction double-ended break case.
Steam Generator Equilibration and Depressurization Steam generator equilibration and depressurization is the process by which secondary side energy is removed from the steam generators in stages. The FROTH computer code calculates the heat removal from the secondary mass until the secondary temperature is saturated at the containment design pressure. After the FROTH calculations, steam generator secondary energy is removed until the steam generator reaches Tsat at the user-specified intermediate equilibration pressure, when the secondary pressure is assumed to reach the actual containment pressure. The heat Containment Functional Design 6.2.1-27
WATTS BAR WBNP-112 removal of the broken loop steam generator and intact loop steam generators are calculated separately.
During the FROTH calculations, steam generator heat removal rates are calculated using the secondary side temperature, primary side temperature, and a secondary side heat transfer coefficient determined using a modified McAdam's correlation (Reference 26). Steam generator energy is removed during the FROTH transient until the secondary side temperature reaches saturation temperature at the containment design pressure. The constant heat removal rate used is based on the final heat removal rate calculated by FROTH. The remaining steam generator energy available to be released is determined by calculating the difference in secondary energy available at the containment design pressure and that at the (lower) user-specifed equilibration pressure, assuming saturated conditions. This energy is then divided by the energy removal rate, resulting in an equilibration time.
Decay Heat Model ANS Standard 5.1 (Reference 25) was used in the LOCA mass and energy release model for Watts Bar Unit 1 for the determination of decay heat energy. This standard was balloted by the Nuclear Power Plant Standards Committee (NUPPSCO) in October 1978 and subsequently approved. The official standard (Reference 25) was issued in August 1979.
The primary assumptions that make this calculation specifc for the Watts Bar Nuclear Plant Unit 2 are the enrichment factor, minimum/maximum new fuel loading per cycle, and a conservative end of cycle core average burnup. A conservative lower bound for enrichment of 3 percent was used. Table 6.2.1-20 lists the decay heat curve used.
Significant assumptions in the generation of the decay heat curve are the following:
- 1. Decay heat sources considered are fission product decay and heavy element decay of U-239 and Np-239.
- 3. Fission rate is constant over the operating history of maximum power level.
- 4. The factor accounting for neutron capture in fission products has been taken from Equation 11, of Reference 25 (up to 10,000 seconds) and Table 10 of Reference 25 (beyond 10,000 seconds).
- 5. The fuel has been assumed to be at full power for 1,096 days.
- 6. The number of atoms of U-239 produced per second has been assumed to be equal to 70 percent of the fssion rate.
- 7. The total recoverable energy associated with one fission has been assumed to be 200 MeV/fssion.
6.2.1-28 Containment Functional Design
WATTS BAR WBNP-112
- 8. Two sigma uncertainty (two times the standard deviation) has been applied to the fission product decay.
Short-Term Mass and Energy Releases The short-term mass and energy release models and assumptions are described in Reference [9]. The LOCA short-term mass and energy release data used to perform the containment analysis given in Sections 6.2.1.3.4 and 6.2.1.3.9 are listed below:
Section Break Size and Location Table 6.2.1.3.4 Double-Ended Cold Leg 6.2.1-23 Guillotine Break Outside the Biological Shield 6.2.1.3.4 Double-Ended Hot Leg 6.2.1-24 Guillotine Break Outside the Biological Shield 6.2.1.3.9 Double-Ended Pressurizer 6.2.1-28 Spray Line Break 6.2.1.3.9 127 in2 Cold Leg Break at the 6.2.1-30 Reactor Vessel 6.2.1.3.7 Accident Chronology For a double-ended pump suction loss-of-coolant accident, the major events and their time of occurrence are shown in Table 6.2.1-25 for the minimum safeguards case.
6.2.1.3.8 Mass and Energy Balance Tables Sources of Mass and Energy The sources of mass considered in the LOCA mass and energy release analysis are given in Table 6.2.1-26a. These sources are the RCS, accumulators, and pumped safety injection.
The energy inventories considered in the LOCA mass and energy release analysis are given in Table 6.2.1-26b. The energy sources include:
RCS water Accumulator water Pumped injection water Decay heat Core-stored energy RCS metal - Primary metal (includes steam generator tubes)
Containment Functional Design 6.2.1-29
WATTS BAR WBNP-112 Steam generator metal (includes transition cone, shell, wrapper, and other internals)
Steam generator secondary energy (includes fluid mass and steam mass)
Secondary transfer of energy (feedwater into and steam out of the steam generator secondary)
It should be noted that the inconsistency in the energy balance tables from the end of reflood to the time of intact loop steam generator depressurization/equilibration ("Total Available" data versus "Total Accountable") resulted from the exclusion of the reactor upper head in the analysis following blowdown. It has been concluded that the results are more conservative when the upper head is neglected. This does not affect the instantaneous mass and energy releases or the integrated values, but causes an increase in the total accountable energy within the energy balance table.
The mass and energy inventories are presented at the following times, as appropriate:
Time zero (initial conditions)
End of blowdown time End of refill time End of reflood time Time of broken loop steam generator equilibration to pressure setpoint Time of intact loop steam generator equilibration to pressure setpoint The chronology of events for the DEPS case is shown in Table 6.2.1-25.
The energy release from the zirc-water reaction is considered as part of the WCAP-1 0325-P-A (Reference 20) methodology. Based on the way that the energy in the fuel is conservatively released to the vessel fluid, the fuel cladding temperature does not increase to the point where the zirc-water reaction is significant. This is in contrast to the 10 CFR 50.46 analyses, which are biased to calculate high fuel rod cladding temperatures and therefore a non-significant zirc-water reaction.
For the LOCA mass and energy calculation, the energy created by the zirc-water reaction value is small and is not explicitly provided in the energy balance tables. The energy that is determined is part of the mass and energy releases and is therefore already included in the LOCA mass and energy release.
The methods and assumptions used to release various energy sources are given in Reference 20.
The consideration of the various energy sources in the mass and energy release analysis provides assurance that all available sources of energy have been included 6.2.1-30 Containment Functional Design
WATTS BAR WBNP-112 in this analysis. Therefore, the review guidelines presented in Standard Review Plan Section 6.2.1.3 have been satisfied.
6.2.1.3.9 Containment Pressure Differentials Consideration is given in the design of the containment internal structures to localized pressure pulses that could occur following a loss-of-coolant accident or a main steam line break. If either type of pipe rupture were to occur in these relatively small volumes, the pressure would build up at a rate faster than the overall containment, thus imposing a differential pressure across the walls of the structures.
These subcompartments include the steam generator enclosure, pressurizer enclosure, and upper and lower reactor cavity. Each compartment is designed for the largest blowdown flow resulting from the severance of the largest connecting pipe within the enclosure or the blowdown flow into the enclosure from a break in an adjacent region.
The following paragraphs summarize the design basis calculations:
Steam Generator Enclosure The worst break possible in the steam generator enclosure is a double-ended rupture of the steamline pipe at no load conditions. Based on an investigation of postulated break locations, the rupture is assumed to occur at the point where the steamline exits the steam generator. The blowdown for this break is given in Table 6.2.1-27a. The TMD computer code (Reference 4) using the compressibility factor and assuming unaugmented critical flow is used to calculate the short-term pressure transient. The nodalization of the steam generator enclosure where the break occurs is shown in Figure 6.2.1-81. Node 51 is the break element and has a flow path to the adjacent steam generator enclosure which is a mirror image of the enclosure where the break occurs. Both enclosures are nodalized in the same manner; their nodal network is shown in Figure 6.2.1-82 and their input data is given in Tables 6.2.1-27b and 6.2.1-27c. This input data assumes that the insulation remains intact. The loss coefficients were computed using Reference [12]. The maximum number of nodes used is based on the geometry of the system. The steam generator compartment is essentially symmetrical with no major obstructions to flow which would introduce asymmetric pressures. In addition, the flow path to the adjacent steam generator is at the top of the enclosure. Therefore, a significant differential pressure will not occur across the steam generator vessel. The balance of plant data is similar to that presented in Section 6.2.1.3.4.
The peak pressure differentials across the steam generator enclosure, the steam generator vessel, and the steam generator separator wall are given in Table 6.2.1-27d.
Figure 6.2.1-83 shows the differential pressure transient between the break element and the upper compartment (Node 25). Figures 6.2.1-84 and 6.2.1-85 illustrate the differential pressure transient across the steam generator vessel. As Figures 6.2.1-84 and 6.2.1-85 show, the pressure differentials across the vessel are low and are due solely to inertial effects. The pressure vs time curve for the break element is given in Containment Functional Design 6.2.1-31
WATTS BAR WBNP-112 Figure 6.2.1-86 and for the upper compartment (Node 25) in Figure 6.2.1-86a (Refer to Section 3.8.3.4.8 for steam generator compartment structural design description).
Pressurizer Enclosure The worst break possible in the pressurizer enclosure is a double-ended rupture of the six-inch spray line. The rupture is assumed to occur at the top of the enclosure. The blowdown for this break is given in Table 6.2.1-28. The TMD computer code using the compressibility factor and assuming unaugmented critical flow is used to calculate the short-term pressure transient. The nodalization of the enclosure is shown in Figure 6.2.1-87. Node 51 is the break element. The input data is given in Table 6.2.1-29a.
This input data assumes that the insulation remains intact. The loss coefficients were computed using Reference [12]. The maximum number of nodes used was based on the geometry of the system. The pressurizer compartment is essentially symmetrical with no major obstructions to flow which would introduce asymmetric pressures on the pressurizer vessel. The balance of plant data is similar to that presented in Section 6.2.1.3.4.
The peak pressure differentials across the pressurizer enclosure's walls, and across the pressurizer vessel are given in Table 6.2.1-29b. Figure 6.2.1-88 shows the pressure transient between the break element and the upper compartment (Node 25).
As Figures 6.2.1-89 through 6.2.1-91 show, the significant pressure differential across the vessel are low, occur early, and are due solely to inertial effects. The pressure vs.
time curve for the break element is given in Figure 6.2.1-92 (Refer to Section 3.8.3.4.9 for pressurizer compartment structural design description).
Reactor Cavity The TMD computer code with the unaugmented homogeneous critical flow correlation and the isentropic compressible subsonic flow correlation was used to calculate pressure transients in the reactor cavity region.
Nodalization sensitivity studies were performed before the analysis was begun. The total number of nodes used varied from 6 to 68. In the 6-element model, no detail of the reactor vessel annulus was involved, and for that reason the model was discarded.
Subsequent model changes primarily involved greater detail in the reactor vessel annulus. First, the annulus was divided into two vertical and eight circumferential regions. Next, some additional detail was added to the region of the broken nozzle.
The next changes were effected by increasing the model to three vertical and eight circumferential regions. The total integrated pressure in the reactor cavity changed only slightly because of the last change. The next change, to 68 elements, produced the model shown with detailed modeling around the nozzle sustaining the break. The additional elements from 48 to 52 are external to the reactor cavity (ice condenser).
Additional elements were added to account for all real area changes in the immediate vicinity of the break (i.e., Elements 53 and 54 were added to model the broken loop pipe annulus and the broken loop inspection port, respectively).
The nodal scheme around the reactor vessel produces a very accurate post accident pressure profile because of its design. Element 3 is a small element inside the primary 6.2.1-32 Containment Functional Design
WATTS BAR WBNP-112 shield. It would contain internal flow losses due to turning and thus contain a pressure gradient if it were made larger. The four elements numbered 33, 34, 45, and 46 are made small to minimize internal pressure variation, and the elements farther from the break are made larger because pressure gradients are low in those regions.
Figure 6.2.1-27 illustrates the positions of some of the compartments. Figure 6.2.1-28 shows the flow path connections for the 68 element model. Figure 6.2.1-29 illustrates the general configuration of the reactor vessel annulus nodalization. In the model, the lower containment is divided into four loop compartments (21 to 24). The upper containment is represented by Compartment 32. The ice condenser is modeled as five elements (48 to 52), neglecting any flow distribution effects. The break simultaneously occurs in Elements 1 and 25, immediately surrounding the nozzle. The corresponding broken loop pipe annulus is represented by Element 53. The lower reactor cavity is modeled by Element 2, the upper reactor cavity by Element 47, and the remainder of the elements, as shown in Figure 6.2.1-29, model the reactor vessel annulus.
Compartments 15, 42, and 16 are really adjoining Compartments 17, 43, and 18, respectively, and Compartment 13 is on the opposite side of the vessel from the assumed break. Element 54 represents the inspection port volume above the break.
A break limiting restraint restricts the break size. A 127 in2 cold leg break is the limiting case break for the reactor cavity analysis. The mass and energy release rates are presented in Table 6.2.1-30. Tables 6.2.1-31 and 6.2.1-32 provide the volumes, flow paths, lengths, diameters, flow areas, resistance factors, and area ratios for the elements and their connections.
The inspection port plugs were assumed to be removed at the start of the accident. All insulation is assumed in place and uncrushed during the entire transient except for the insulation between the break and the reactor vessel annulus. This insulation was conservatively assumed to crush to zero thickness.
The loss coefficient (k) values were determined by changes in flow area and by turns the flow makes in traveling from the centroid of the upstream node to the centroid of the downstream node. The k and f factors for each path were determined using methods from such references as "Flow of Fluids through Valves, Fittings, and Pipes" by the crane company and "Chemical Engineering" by J. M. Coulson and J. A.
Richardson.
Figures 6.2.1-30 through 6.2.1-68 show representative pressure transients for the break compartments, the upper and lower reactor cavities, the inspection port volume and pipe annulus near the break, the upper containment and the reactor vessel annulus. These plots demonstrate that the pressure gradient is steep near the break location and is very gradual farther away from the break. This indicates that the model must be very detailed close to the break location, but less detail is required with increasing distance (Refer to Section 3.8.3.5.3 for reactor cavity structural design description).
Containment Functional Design 6.2.1-33
WATTS BAR WBNP-112 6.2.1.3.10 Steam Line Break Inside Containment Pipe Break Blowdowns - Spectra and Assumptions A series of steam line breaks was analyzed to determine the most severe break condition for containment temperature and pressure response. The following assumptions were used in these analyses.
(1) The following break types were evaluated.
(a) Double-ended 4.6 ft2 ruptures occurring at the nozzle on one steam generator. Steam line flow restrictors in the steam generators limit the effective break area of a full double-ended pipe rupture to a maximum of 1.4 ft2 per steam generator.
(b) The largest split break which will not generate the low steamline pressure signal for steamline isolation.
(c) Small split breaks of 0.6, 0.35, and 0.1 ft2.
(2) Steam line isolation signals and feedwater line isolation signals are generated by either a low steam line pressure signal, high or high-high containment pressure signal, or high steam line pressure rate signal. An allowance of 8 seconds is assumed for steam line isolation including generation, processing, and delay of the isolation signal and valve closure.
An allowance of 8 seconds is assumed for feedwater line isolation including generation, processing, and delay of the isolation signal and valve closure.
(3) Failure of a diesel generator is assumed in the containment model for all cases. This results in the loss of one containment safeguards train resulting in minimum heat removal capability. There is no diesel failure associated with the steam line break model.
(4) Blowdown from the broken steam line is assumed to be dry saturated steam.
(5) Plant power levels of 100.6% and zero of nominal full-load power for DER, and split pipe ruptures at 30% of nominal full-load power.
(6) Failure of a main steamline isolation valve (MSIV), failure of a feedwater isolation valve (FIV) or control valve (FCV), failure of auxiliary feedwater runout control protection, and failure of a safety injection train are considered.
(7) The auxiliary feedwater system is manually realigned by the operator after 10 minutes to terminate AFW to the faulted steam generator.
6.2.1-34 Containment Functional Design
WATTS BAR WBNP-112 (8) For the full double-ended ruptures, the main feedwater flow to the steam generator with the broken steam line was calculated based on an initial flow of 100% of nominal full power flow and a conservatively rapid steam generator depressurization. The peak value of this flow occurring just prior to isolation is 328% of nominal.
Break Flow Calculations (1) Steam Generator Blowdown Break flows and enthalpies from the steam generators are calculated using the Westinghouse LOFTRAN code[14]. Blowdown mass and energy release are determined using the LOFTRAN code which includes effects of core power generation, main and auxiliary feedwater additions, engineered safeguards systems, reactor coolant system thick metal heat storage, and reverse steam generator heat transfer.
(2) Steam Plant Piping Blowdown The contribution to the mass and energy releases from the secondary plant steam piping is included with the mass and energy release rates presented in Table 6.2.1-39. For all ruptures, the steam piping volume blowdown begins at the time of the break and continues at a uniform rate until the entire piping inventory is released. The flowrate is determined using the Moody correlation, the pipe cross-sectional area, and the initial steam pressure.
Following the piping blowdown, reverse flow from the intact steam generators continues to simulate the reverse steam generator flow until steam line isolation.
Single Failure Effects (1) Failure of the main steam isolation valve (located outside of containment) in the steam line with the break allows steam from all four main steam lines (downstream of the other main steam isolation valves which close) to flow out the break. The analysis accounts for this effect by including an allowance for additional mass and energy released through the break due to the volume of steam contained in the main steam lines. No additional steam is released through the break if the postulated single failure is a main steam isolation valve in another steam line not closing. In this case, the main steam isolation valve in the broken steam line does close and there is no backflow from the downstream piping to the break.
(2) Failure of a feedwater isolation valve could only result in additional inventory in the feedwater line which would not be isolated from the steam generator.
The mass in this volume can flash into the steam generator and exit through the break. The feedwater regulating valve closes in no more than 6.5 seconds precluding any additional feedwater from being pumped into the Containment Functional Design 6.2.1-35
WATTS BAR WBNP-112 steam generator. The additional line volume available to flash into the steam generator is that between the feedwater isolation valve and the feedwater regulating valve.
(3) Failure of a feedwater control valve to operate properly can result in an increased feedwater flow into the steam generator and exit through the break.
Feedwater isolation valve closure limits the feedwater addition to the steam generator.
(4) Failure of the auxiliary feedwater runout control equipment would result in higher auxiliary feedwater flows entering the steam generator prior to realignment of the auxiliary feedwater system. For cases where the runout control operates properly, a constant auxiliary feed flow of approximately 1,500 gpm was assumed. This value was increased to approximately 2,250 gpm for the 100% and 0% power cases and 2040 gpm for the 30% power cases to simulate a failure of the runout control.
(5) Failure of a safety injection train results in less SI flow and will result in a greater return to power. For consistency, with the steam line break core response analysis, the steam line break mass and energy model conservatively assumes failure of a safety injection train.
Worst-Case Mass and Energy Releases The following steam line break cases were determined to represent the worst case steamline break results.
(1) Full double-ended rupture at 100.6% of nominal full power with a failure of the AFW runout control system. This represents the limiting DER case in terms of calculated peak temperature.
(2) A 0.6 ft2 split break at 30% of nominal full power with a failure of the AFW runout control system. This represents the limiting SB case in terms of calculated peak temperature.
(3) A 0.35 ft2 split break at 30% at nominal full power with a failure of the AFW runout control system. This represents the limiting SB case in terms of superheat temperature duration.
Mass and energy releases for these cases are listed in Table 6.2.1-39.
Maximum Containment Temperature Analysis for Steam Line Break Following a steam line break in the lower compartment of an ice condenser plant, two distinct analyses must be performed. The first analysis, a short-term pressure analysis, has been performed with the TMD computer code (see Section 6.2.1.3.9).
The second analysis, a long-term analysis, does not require the large number of nodes 6.2.1-36 Containment Functional Design
WATTS BAR WBNP-112 which the TMD analysis requires. The computer code which performs this analysis is the LOTIC computer code.
The LOTIC-3 computer code was developed to analyze steamline breaks in an ice condenser plant. Details of the LOTIC-3 computer code are given in Reference [3]. It includes the capability to calculate superheat conditions, and has the ability to begin calculations from time zero. The LOTIC-3 computer code has been found to be acceptable for the analysis of steam line breaks[3] with the following restrictions.
(1) Mass and energy release rates are calculated with an approved model.
(2) Complete break spectrums are analyzed.
(3) Convective heat flux calculations, as described in References [2] and [27],
are performed for all break sizes.
For the worst case steam line breaks, one condensation model is used by the LOTIC-3 computer code. For these three breaks, the conservative 0% condensate reevaporization and convective heat flux model is used.
Containment Transient Calculations The following are the major input assumptions used in the LOTIC-3 steamline break analysis for the Watts Bar Nuclear Plant.
(1) Minimum safeguards are employed, e.g., one of two spray pumps, and one of two air return fans.
(2) A quantity of 2.125x106 lbs of ice is assumed for the steamline break cases to be initially in the ice condenser.
(3) The boron injection tank remains installed without heat tracing, and the boric acid concentration is reduced to zero ppm (Table 6.2.1-40).
(4) The air return fan is effective 10 minutes after the transient is initiated. Actual air return fan initiation can take place in 9+1 minutes. Initiation as early as 8 minutes does not adversely affect the outcome of the analysis.
(5) A uniform distribution of steam flow into the ice bed is assumed.
(6) The initial conditions in the containment are a temperature of 120°F in the lower compartment, 120°F in the dead-ended compartment, a temperature of 85°F in the upper compartment, and a temperature of 32°F in the ice condenser. All volumes (see Table 6.2.1-13) are at a pressure of 0.3 psig .
(7) A containment spray pump flow of 4,000 gpm is conservatively used in the upper compartment. A diesel loading sequence for the containment sprays to energize and come up to full flow and head in 234 seconds was used in the analysis.
Containment Functional Design 6.2.1-37
WATTS BAR WBNP-112 (8) Containment structural heat sinks as presented in Table 6.2.1-1 were used.
The material properties are given in Table 6.2.1-5.
(9) The air return fan empties air at a rate of 40,000 ft3/min from the upper to the lower compartments. The total calculated air flow rate discharged to the dead-end compartment used is 41,885 cfm and is, therefore, bounded.
(10) A series of large break cases (1.4 ft2 double-ended ruptures) was run to determine the limiting large break case (Table 6.2.1-41). In addition, a series of small breaks was analyzed with LOTIC at the 30% power level (Table 6.2.1-42).
(11) The mass and energy releases for the limiting breaks are given in Table 6.2.1-39. Since these rates are considerably less than the RCS double-ended breaks and their total integrated energy is not sufficient to cause icebed meltout, the containment pressure transients generated for the RCS breaks will be more severe. However, since the steam line break blowdowns are superheated, the lower compartment temperature transients calculated in this analysis will be limited. These temperature transients are given in Figures 6.2.1-69 through 6.2.1-74.
(12) The heat transfer coefficients to the containment structures are based on the work of Tagami. An explanation of their manner of application is given in Reference [3]. The stagnant heat transfer coefficients were limited to 72 Btu/hr-ft2. This corresponds to a steam-air ratio of 1.4 (according to the Tagami correlation). The imposition of this limitation is to restrict the use of the Tagami correlation within the range of steam-air ratios from which the correlation was derived.
The containment responses presented identify the limiting and most severe cases for the large double-ended ruptures and small split breaks.
Large Break The limiting case among the double-ended ruptures, which yielded a calculated peak temperature of 323.9°F and a peak pressure of 9.29 psig, is the 1.4 ft2 loop break at 100.6% of nominal full power with a failure of the AFW runout control system. Figure 6.2.1-69 provides the upper and lower compartment temperature transients, and Figure 6.2.1-70 illustrates the lower compartment pressure transients. Table 6.2.1-39 contains the mass and energy release rates for the above case.
Small Break The most severe transient in terms of superheat temperature duration for the small break spectrum is the 0.35 ft2, 30% nominal full power, with AFW pump runout protection failure. The temperature transient with a peak temperature of 324.4°F and peak pressure of 6.58 psig for the case is presented in Figure 6.2.1-71, and the pressure transient is provided in Figure 6.2.1-72. Table 6.2.1-39 provides the mass and energy release rates for this case.
6.2.1-38 Containment Functional Design
WATTS BAR WBNP-112 The most limiting case in terms of peak calculated temperature is the 0.6 ft2, 30%
power, with AFW pump runout protection failure. This case resulted in a calculated peak temperature of 325.1°F and peak pressure of 6.83 psig. Figure 6.2.1-73 presents the temperature transient, and Figure 6.2.1-74 shows the pressure transient of the lower compartment. The mass and energy releases are provided in Table 6.2.1-39.
Tables 6.2.1-43 and 6.2.1-44 provide the overall results of the calculated peak temperatures for the large and small break spectrums, respectively.
6.2.1.3.11 Maximum Reverse Pressure Differentials Following a postulated pipe break accident, the occurrence inside the ice condenser containment may be characterized by two distinct periods:
(1) The initial blowdown, which occurs in approximately 10 seconds. During this period, the air initially in the lower compartment is swept into the upper compartment and the dead-ended compartment by the blowdown mass.
Large mass and pressure gradients occur throughout the containment.
(2) The depressurization and post-blowdown period which occurs after the end of the initial blowdown. During this period the pressure gradient within the four compartments (upper, lower, ice condenser, and dead-ended) is almost nonexistent. The shape of the pressure transient resembles that of the mass and energy releases. Pressure decreases as blowdown diminishes, followed by a slow increase sometime during the reflood.
The analysis for the first period will usually require the modeling of the containment into many nodes so that the non-uniformity of pressure and mass distribution may be properly represented. This has been done in the TMD code.
On the other hand, the analysis for the second period will only require the modeling of the containment by a four-compartment system. These calculations are performed by the LOTIC code [1, 28].
The code options and features discussed are used in calculating ECCS back-pressure and reverse pressure differentials across the operating deck.
Basic Assumptions (1) The containment is assumed to be physically divided into four compartments:
upper, lower, ice condenser, and dead-ended compartments. Each compartment is a control volume of uniform temperature, pressure and mass distribution. Steam is also assumed to be saturated in each control volume.
(2) Flow between compartments is related to the pressure differential between the compartments by a flow resistance factor.
(3) A two-sump model is assumed. Temperature is considered to be uniform in each sump.
Containment Functional Design 6.2.1-39
WATTS BAR WBNP-112 Conservation Equations For each control volume or compartment, the conservation equations of mass, energy, momentum, and volume, an ideal gas law for air, and the equation of state for saturated steam may be written:
(1) Energy equation:
d- ( V as + V c ) d ( P s + P a )
(M a h a + M s h s + M c h c) - --------------------------- ------------------------------ + ( mh ) out - ( mh ) in = R e dt J dt For the lower compartment:
Re = [Rate of energy out of break]
+ [Rate of flow energy from accumulator in the form of steam, water, and nitrogen]
- [Rate of structural heat removal]
- [Rate of flow energy of sprays if applicable]
- [Rate of heat transfer to the sump]
- [Rate of heat removal by the ice condenser drain flow, if acting as a spray]
- [Rate of energy associated with the loss on condensate from atmosphere falling to floor]
+ [Net rate of flow energy from the dead-ended compartment]
For the upper compartment:
Re = [Flow energy of the entering spray]
- [Structure heat removal rate]
- [Energy rate associated with condensate falling from atmosphere]
For the ice condenser:
Re =[Structure heat removal rate]
- [Rate of heat transfer to the ice]
- [Energy rate associated with ice melt and steam condensate falling from atmosphere]
(2) Conservation of steam and water masses:
dM s dM c
+ ----------- + ( M s ) - ( M s ) in = R s dt dt out 6.2.1-40 Containment Functional Design
WATTS BAR WBNP-112 For the lower compartment:
Rs = [Rate of flow out of the RCS]
+ [Rate of flow out of the accumulator in the form of steam and water]
+ [Flow rate of the entering spray if applicable]
- [Rate of condensate falling to the floor]
+ [Rate of steam flow from the dead-ended compartment]
For the upper compartment:
Rs = [Flow rate of the entering spray]
- [Rate of condensate falling to the floor]
For the ice condenser:
Rs = - [Rate of condensate falling to the floor]
(3) Conservation of air mass:
dM
a- + ( M a ) - ( M a ) in = R a dt out For the lower compartment:
Ra = [Rate of nitrogen flow out of the accumulator]
+ [Rate of air flow out of the dead-ended compartment]
For the upper compartment and the ice condenser:
Ra = 0 (4) Conservation of momentum:
2 1 K M ij P i - P j = --- -----ij- ---------
2 A 2 g c
(5) Volume conservation:
dV as dV c
+ ---------- = R v dt dt Containment Functional Design 6.2.1-41
WATTS BAR WBNP-112 For the lower compartment:
Rv = [Rate of increase in sump water volume]
For the upper compartment:
Rv = 0 For the ice condenser:
Rv = [Rate of increase in free volume due to ice melting]
(6) Ideal gas law for air:
PaVas = MaRaT (7) Equations of state for saturated steam:
Ps = f1(T), hs = f2(T), vs = f3(T)
For the dead-ended compartment, the structure heat removal is assumed to be negligible, and the conservation equations of energy and mass simplified to:
d v d ( Ps + Pa )
( M a h a + M s h s ) - --- ---------------------------
- = [ Rate of energy flow from the lower compartment ]
dt J dt
( dM a )
= [Rate of air flow from the lower compartment]
dt
( dM s )
= [Rate of steam flow from the lower compartment]
dt Method of Solution The preceding equations were linearized and programmed for simultaneous solutions using the standard Gauss-Jordan reduction method. For each time step, the solutions are the rates of increase of mass and pressure for each constituent in each compartment, and the flow rates between the compartments. These rates are used to control the time step so that total change of the compartment conditions in each time step can be controlled. This assures more accurate and stable solutions.
Structure Heat Transfer The standard Westinghouse ECCS containment structural heat transfer model is applied to this code. This model assumes one dimensional conduction heat transfer in the structure and uses film heat transfer coefficient based primarily on the work of Tagami. The Tagami correlation for the film heat transfer may be written as:
6.2.1-42 Containment Functional Design
WATTS BAR WBNP-112 E 0.6 H max = 75 -------- (1) tp V t
H = H max = -------- for 0 t t p (2) tp
- 0.5 [ t - t p ]
H = H stag + [ H max - H stag ]e for t p t (3) where:
H stag = 2 + 50 X (4)
For this application, we have found it is useful to relate the "coolant energy transfer",
(E/tpV), to containment conditions. This may be done by writing:
E Ms hs + Mf hf 1 M
- = ---------- h s + -------f h f
= ------------------------------- (5) tp V tp V tp vs Ms where:
h s, h f and vs are respectively the enthalpies of saturated steam and water, and the specific volume of steam, at tp, the time when the peak containment pressure is reached.
Equations (1) through (5) are used for the lower compartment structure calculations.
For the upper compartment, only the stagnant heat transfer correlation of Equation (4) is used because of little steam penetration into the upper compartment even during the initial blowdown period.
Ice Condenser Heat Transfer The transfer of heat from steam to ice which results in the simultaneous occurrence of steam condensation and ice melting is a complex mechanism.
During the initial blowdown period when high temperature blowdown steam and water hits the bottom of ice columns, and then flows over the ice surface, turbulent condensation results. During this period the heat transfer rate is strongly dependent on the thickness of the liquid film which separates the high temperature blowdown masses from the ice. This liquid film is composed of steam condensate and ice melt.
On the macroscopic scale, this is the only heat transfer resistance and the Containment Functional Design 6.2.1-43
WATTS BAR WBNP-112 effectiveness of the ice condenser is determined by the rate which this liquid film may be withdrawn. A semi-empirical model for the ice condenser heat transfer during this period is available and has been used successfully in the TMD code. The LOTIC code is not intended to duplicate this effort. Instead mass and energy balances are used to calculate the total ice melting during this period. Following the initial blowdown period, there is a transition period when the blowdown mass and energy rates are decreasing rapidly and the containment atmosphere as a whole is losing internal energy.
Depressurization and decreasing compartment temperature generally characterize this transition period. As the containment conditions lapse into a much more stable and slowly changing pace after the transition period, the blowdown from the broken pipe is almost drawing to an end. Flow in the ice condenser is now at a rate which is almost negligible compared to that in the initial blowdown period. Temperature in the ice condenser atmosphere has also decreased. Thus, heat transfer is governed by combining natural convection and steam diffusion through an almost stagnant atmosphere. Due to the large air content, the resistance to diffusion is large.
Therefore, most of the temperature difference between the free-steam steam-air mixture and the ice occurs between the free-steam and the free surface of the liquid film. Temperature difference across the liquid film is now comparatively small. Due to the loss of dominance for the liquid film resistance in the overall heat transfer mechanism, it is not surprising for Yen, Zender, Zavohik, and Tien[11] to conclude that ice melting has very little effect on the overall heat transfer coefficient for condensation-melting heat transfer in the presence of a substantial air concentration. From this, we may therefore treat the ice as if it were simply a cold structure and use Equation (4) to calculate the heat transfer coefficient after the transition period.
During the transition period, it is plausible to assume that the ice condenser is capable of maintaining its internal energy by condensing any excess energy which flow into the ice condenser.
Special Code Capabilities in Response to Previous NRC Concerns (1) Heat removal from the lower compartment by the ice condenser drain may be accounted for by input of a spray-like efficiency.
(2) Heat transfer between the lower compartment atmosphere and the sump surface can also be taken into account.
Drains are provided at the bottom of the ice condenser compartment to allow the melt/condensate water to flow out of the compartment during a loss of coolant accident. In the modified LOTIC code, a calculation of the flow rate at which water leaves these ice condenser drains is included. The solution was reached by using the hydraulic incompressible flow equations commonly found in the literature for both filled pipe flow and fall (weir) flow conditions and at any point in time using the minimum flow rate calculated by the two methods. The filled pipe flow equation employed was a simplified Bernoulli balance:
6.2.1-44 Containment Functional Design
WATTS BAR WBNP-112 2
V Z 1 = ----- + h f + Z 2 2g where:
Z = Elevation V = Velocity g = Gravitational constant
= Density V 22 fl- ------
hf = -----
- g sd 2 Subscripts 1 and 2 represent conditions at the inlet and outlet of the drain, respectively.
The area of the ice condenser sump was taken to be 3170 ft2, and the height of the door sill to be 8.75 inches. After calculating the velocity from the previous equation, the mass flow rate can be calculated from
- = V A m 2 2 Since a filled pipe flow condition may not exist during the entire post accident transient, a calculation of the draining rate based on the existence of a fall flow phenomena was included. The corresponding equations are outlined below, 2
Q = --- 2g ( H e3 2 - h 13 2 )
3 where:
Q = Discharge per foot of width (ft3/sec-ft)
He = Energy of fluid upstream of the fall h1 = Energy of the fluid at the fall edge minus the flowing height D1 = 0.643 Dc h1 = He - D1 By assuming the approach velocity equals zero and through substitution, we arrive at the simplified equation:
Containment Functional Design 6.2.1-45
WATTS BAR WBNP-112 2
Q = --- 2g [ D c3 2 - ( 0.357 D c) 3 2]
3 or Q = 4.2088 D c3 2 where:
Dc = ft.
Calculation of Maximum Reverse Pressure Differential The computer model previously described was used to calculate the reverse differential pressure across the operating deck. In order to calculate a maximum reverse differential pressure the following assumptions were made:
(1) The dead-ended compartment volumes adjacent to the lower compartment (fan and accumulator rooms, pipe trenches, etc.) were assumed to be swept of air during the initial blowdown. This is a very conservative assumption, since this will maximize the air mass forced into the upper ice bed and upper compartment thus raising the compression pressure. In addition, it will minimize the mass of the noncondensables in the lower compartment. With this modeling the dead-ended volume is included with that of the lower compartment (see Figure 6.2.1-75), resulting in a 3-volume simulation of the containment.
(2) The minimum containment temperatures are assumed in the various subcompartments. This will maximize the air mass forced into the upper containment. It will also increase the heat removal capability of the cold lower compartment structures.
(3) An RWST temperature of 100°F is assumed. This will help raise the upper containment temperature and pressure higher for a longer period of time. The current maximum RWST temperature is 105°F, which has a negligible effect.
(See Table 6.2.1-37.)
(4) The upper containment spray flowrates used were runout flows.
(5) Containment spray to the upper compartment was assumed to start at 25 seconds. An early start time is conservative in that it raises the upper compartment temperature and pressure when the air mass in the upper compartment is at its highest value. Containment spray initiation to the upper containment is tabulated in Table 6.2.1-25. An increased delay should have no negative effect on the maximum reverse pressure differential.
(6) The containment geometry is the same as that used in the minimum pressure analysis for ECCS purposes. (See Tables 6.2.1-33 through 6.2.1-36.)
6.2.1-46 Containment Functional Design
WATTS BAR WBNP-112 (7) The Westinghouse ECCS model (see WCAP-8339) was used for heat transfer to the structure.
(8) The mass and energy releases used are based on the analysis presented in WCAP-8479.
(9) Ice condenser doors are assumed to act as check valves, allowing flow only into the ice condenser.
(10) The loss coefficient (k/A2) of the deck fins for air flow from the upper to the lower compartment was taken to be 0.0072 ft-4. This value was based on the capabilities of the fans while running. With the fans not running the loss coefficient would be 0.0278 ft-4.
With these assumptions the maximum reverse pressure differential across the operating deck was calculated to be 0.65 psi. The following plots have been provided:
Figure 6.2.1-76 which shows upper and lower compartment pressures.
Figure 6.2.1-77 which shows upper and lower compartment temperatures.
Figure 6.2.1-78 which shows upper to lower compartment flowrates.
Parametric studies have been made with this model. Various effects have been investigated to determine changes in the maximum reverse pressure differential.
Table 6.2.1-37 gives some of these studies with their results. For Case 6, Figures 6.2.1-79 and 6.2.1-80 give plots similar to Figures 6.2.1-76 and 6.2.1-77. Presented in Table 6.2.1-38, also for Case 6, are the sump temperature and the steam exit flow from the ice condenser, both as a function of time.
Significant margin exists between the design reverse differential pressures across the operating deck and the ice condenser lower inlet doors and those calculated pressures presented in Table 6.2.1-37.
Nomenclature SYMBOL DESCRIPTION A Flow area E Total energy J Conversion constant, 778 ft-lbf/Btu K Flow resistance factor M Mass P Pressure R Gas constant R Rate Containment Functional Design 6.2.1-47
WATTS BAR WBNP-112 SYMBOL DESCRIPTION T Temperature V Volume gc Conversion constant, 32.2 ft-lbm/lbf-sec2 h Enthalpy m Mass flow rate between two compartments t Time x Steam-air ratio v Specific volume Density SUBSCRIPT a Air as Air and steam c Suspended or entrained water e Energy i i-th compartment j j-th compartment ij from i-th compartment to j-th compartment s Steam REFERENCES (1) Long Term Ice Condenser Containment Code - LOTIC Code, WCAP-8354-P-A, April 1976 (Proprietary), WCAP-8355A, April 1976 (Non-proprietary).
(2) "Final Report Ice Condenser Full-Scale Section Tests at the Waltz Mill Facility", WCAP-8282, February 1974 (Proprietary).
(3) Westinghouse Long-Term Ice Condenser Containment Code - LOTIC-3 Code, WCAP-8354-P-A S2, February 1979 (Proprietary), WCAP-8355-NP-S2, February 1979 (Non-Proprietary).
(4) "Ice Condenser Containment Pressure Transient Analysis Method,"
WCAP-8078, March 1973 (Non-Proprietary).
6.2.1-48 Containment Functional Design
WATTS BAR WBNP-112 (5) Test Plans and Results for the Ice Condenser System, Ice Condenser Full-Scale Section Test at the Waltz Mill Facility, WCAP-8110-S6, May 1974 (Non-proprietary).
(6) Deleted by Amendment 85.
(7) Deleted by Amendment 85.
(8) Deleted by Amendment 85.
(9) Topical Report Westinghouse Mass and Energy Release Data for Containment Design, WCAP-8264-P-A, Rev. 1, August 1975 (Proprietary),
WCAP-8312-A, Rev. 2 (Non-proprietary).
(10) Deleted by Amendment 85.
(11) Yen, Y. C., Zender, A., Zavohik, S. and Tien, C., "Condensation - Melting Heat Transfer in the Presence of Air," Thirteenth National Heat Transfer Conference, AICHE - ASME Denver.
(12) Crane Technical Paper #410, "Flow of Fluid."
(13) "Electrical Hydrogen Recombiner for PWR Containments," WCAP-7709-P-A (Proprietary) and WCAP-7820-A (Non-Proprietary) and Supplements 1, 2, 3, and 4.
(14) Burnett, T. W. T., et al, "LOFTRAN Code Description," WCAP-7907-P-A (Proprietary), April 1984, WCAP-7907-A (Non-Proprietary), April 1984.
(15) King, H. W., "Handbook of Hydraulics," 4th Edition, 1954.
(16) Deleted by Amendment 97.
(17) Deleted by Amendment 97.
(18) Deleted by Amendment 97.
(19) US NRC Regulatory Guide 1.7, Rev. 2, November 1978, "Control of Combustible Gas Concentrations in Containment Following a Loss of Coolant Accident."
(20) "Westinghouse LOCA Mass and Energy Release Model for Containment Design March 1979 Version," WCAP-10325-P-A, May 1983 (Proprietary),
WCAP-10326-A May 1983 (Non-proprietary).
(21) Interim Report on Safety Assessments and Facilities Establishment Project in Japan for Period Ending June 1965 (No. 1), Tagami, Takasi.
Containment Functional Design 6.2.1-49
WATTS BAR WBNP-112 (22) "Topical Report Westinghouse ECCS Evaluation Model 1981 Version,"
WCAP-9220-P-A, Revision 1, February 1982 (Proprietary), WCAP-9221-A, Revision I, February 1982 (Non-Proprietary).
(23) Docket No. 50-315, "Amendment No. 126, Facility Operating License No.
DPR-58 (TAC No. 71062), D. C. Cook Nuclear Plant Unit 1," June 9, 1989.
(24) Mixing of Emergency Core Cooling Water with Steam: 1/3-Scale Test and Summary, WCAP-8423, June 1975 (Proprietary).
(25) ANSI/ANS-5.1-1979, American National Standard for Decay Heat Power in Light Water Reactor, August 29, 1979.
(26) W. H. McAdams, Heat Transmission, McGraw-Hill 3rd edition, 1954, p. 172.
(27) Answers to AEC Questions on Report WCAP-8282, WCAP-8282-AD1, May 1974 (Proprietary).
(28) Long Term Ice Condenser Containment Code - LOTIC Code, WCAP-8354-P-A-S1, April 1976 (Proprietary), WCAP-8355-A-S1, April 1976 (Non-proprietary).
6.2.1-50 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-1 Structural Heat Sinks (Page 1 of 2)
A. Upper Compartment Area Thickness Material (ft2) (ft)
- 1. Operating Deck Slab 1 4880 1.066 Concrete Slab 2 18280 0.0055 Paint 1.4 Concrete Slab 3 760 0.0055 Paint 1.5 Concrete Slab 4 3840 0.0208 Stainless Steel 1.5 Concrete 2.Shell and Misc Slab 5 56331 0.001 Paint 0.079 Steel B. Lower Compartment
- 1. Operating Deck, Crane Wall, and Interior Concrete Slab 6 31963 1.43 Concrete
- 2. Operating Deck Slab 7 2830 0.0055 Paint 1.1 Concrete Slab 8 760 0.0055 Paint 1.75 Concrete
- 3. Interior Concrete and Stainless Steel Slab 9 2270 0.0208 Stainless Steel 2.0 Concrete
- 4. Floor*
Slab 10 15921 0.0055 Paint 1.6 Concrete
- 5. Misc Steel Slab 11 28500 0.001 Paint 0.0656 Steel Containment Functional Design 6.2.1-51
WATTS BAR WBNP-112 Table 6.2.1-1 Structural Heat Sinks (Page 2 of 2)
Area Thickness Material (ft2) (ft)
C. Ice Condenser
- 1. Ice Baskets Slab 12 149,600 0.00663 Steel
- 2. Lattice Frames Slab 13 75,865 0.0217 Steel
- 3. Lower Support Structure Slab 14 28,670 0.0587 Steel
- 4. Ice Condenser Floor Slab 15 3,336 0.0055 Paint 0.33 Concrete
- 5. Containment Wall Panels & Containment Shell Slab 16 19,100 1.0 Steel & Insulation 0.0625 Steel Shell
- 6. Crane Wall Panels and Crane Wall Slab 17 13,055 1.0 Steel & Insulation 1.0 Concrete
- In contact with sump.
6.2.1-52 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-2 Pump Flow Rates Vs. Time (Time Sequence to Switchover from Injection to Recirculation)
Time after HHSI RHR CSS RHR Safeguards Pump Pump Pump Spray Sump RWST Initiation CCP Flow Flow Flow Flow Flow Flowrate Flowrate (sec) (gpm) (gpm) (gpm) (gpm) (gpm) (gpm) (gpm)
SI Signal 0 0 0 0 0 0 0 0 Initiated CCP Starts and 12 560 0 0 0 0 0 560 Reaches Rated Flow HHSI Pump 17 560 675 0 0 0 0 1235 Starts and Reaches Rated Flow RHR Pump Starts 22 560 675 5500 0 0 0 6735 and Reaches Rated Flow CSS Pump Starts 234 560 675 5500 4950 0 0 11685 and Reaches Rated Flow RWST Low Level 1207.3 560 675 5500 4950 0 0 11685 Alarm, Automatic Realignment of RHR Sump Valves 1267.3 560 675 2750 4950 0 2750 6185 Open, RWST to RHR Valves Close HHSI & CCP 1344.3 560 675 2750 4950 0 2750 4950 Suction Valves from RHR Discharge Open Low-Low RWST 2588.7 560 675 2750 4950 0 2750 4950 Level Alarm Shut Off CSS 2598.7 560 675 2750 0 0 2750 0 Pump Restart CSS 2718.7 560 675 2750 0 0 2750 0 Pump Start RHR Spray 3600 560 675 2750 4950 2000 2750 0 Containment Functional Design 6.2.1-53
WATTS BAR WBNP-112 Table 6.2.1-3 Energy Balances Approx. End of Blowdown Approx. End of Reflood Sink (t = 10.0 sec) (t=243.4 sec)
(Millions of BTUs)
Ice Heat Removal* 190.811 246.406 Structural Heat Sinks* 17.686 57.676 RHR Heat Exchanger Heat Removal* 0.0 0.0 Spray Heat Exchanger Heat Removal* 0.0 0.0 Energy Content of Sump** 173.409 229.192 Ice Melted (millions of lbm) 0.6160 0.8386
- Integrated Heat Rates
- Energy Content of Sump Includes Active and Inactive Regions 6.2.1-54 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-4 Energy Balances Ice Meltout Time Approx. Time of Approx. Peak Pressure (t=2659.8 sec) (t=4348.6 sec)
(Millions of BTUs)
Ice Heat Removal* 601.367 601.389 Structural Heat Sinks* 68.084 100.780 RHR Heat Exchanger Heat Removal* 18.566 38.875 Spray Heat Exchanger Heat Removal* 0.0 32.176 Energy Content of Sump** 597.741 595.857 Ice Melted (millions of lbs) 2.2599 2.2600
- Integrated Heat Rates
- Energy Content of Sump Includes Active and Anactive Regions Containment Functional Design 6.2.1-55
WATTS BAR WBNP-112 Table 6.2.1-5 Material Property Data Thermal Conductivity Volumetric Heat Material Btu/hr-ft-°F Btu/ft3-°F Paint on Steel 0.21 19.9 Paint on Concrete 0.083 39.9 Concrete 0.8 31.9 Stainless Steel 9.4 53.68 Carbon Steel 26.0 53.9 Carbon Steel* 26.0 56.4 Concrete* 0.8 28.8 Insulation on steel (containment walls)* 0.15 2.75 Insulation on steel (crane walls)* 0.20 3.663
- Located in Ice Condenser Compartment 6.2.1-56 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-6 TMD Input for Watts Bar Initial Volume PSteam PAir Temperature Element (ft3) (psia) (psia) (°F) 1 28700. 0.3 14.7 120.
2 36800.
3 70200.
4 38800.
5 36800.
6 25114.
25 651000. 0.3 14.7 120 26 11700.
27 17900.
28 11200.
29 18700.
30 11200.
31 18000. 0.3 14.7 120.
32 10100.
33 15300.
34 13000.
35 4400.
36 4400.
37 9300.
50 1400.
0.3 14.7 120.
Containment Functional Design 6.2.1-57
WATTS BAR WBNP-112 Table 6.2.1-7 TMD Flow Input Data For Watts Bar (Page 1 of 2)
Flow Path Element to Flow Path Length Flow Area Loss Element (ft) (ft2) Coefficient K Area Ratio a/A 1 to 33 6.5 22 1.5 0.048 2 to 27 3.5 48 4.2 0.027 3 to 33 10.2 64 1.5 0.048 4 to 33 7.9 44 1.5 0.048 5 to 31 3.5 42 4.2 0.027 6 to 33 5.7 16 1.5 0.048 26 to 27 9.0 23 2.7 0.067 27 to 3 9.3 46 4.2 0.027 28 to 27 9.0 23 2.7 0.067 29 to 36 3.7 15 3.0 0.044 30 to 31 9.0 23 2.7 0.067 31 to 6 11.0 58 4.2 0.027 32 to 31 9.0 23 2.7 0.067 33 to 5 7.8 36 1.5 0.048 34 to 26 6.6 59 1.5 0.171 35 to 28 2.8 17 1.5 0.049 36 to 30 2.8 17 1.5 0.049 37 to 32 3.2 23 1.5 0.067 50 to 4 3.6 1.6 1.5 0.002 50 to 4 3.9 2.5 1.5 0.002 50 to 30 3.8 6.8 1.5 0.067 1 to 2 17.5 550 0.33 0.43 2 to 3 24.2 550 0.33 0.43 3 to 4 22.3 600 0.30 0.47 4 to 5 19.7 550 0.33 0.43 5 to 6 17.2 550 0.33 0.43 6 to 1 29.4 140 1.32 0.09 26 to 32 71.0 126 1.6 0.843 27 to 1 6.9 60 4.2 0.027 28 to 26 80.0 146 0.5 0.977 29 to 35 3.8 15 3.0 0.044 30 to 28 51.0 81 1.6 0.542 31 to 4 9.3 44 4.2 0.027 32 to 30 80.0 146 0.5 0.977 33 to 2 8.1 38 1.5 0.048 34 to 27 4.5 17 3.0 0.049 35 to 27 3.7 15 3.0 0.044 36 to 31 3.1 10 3.0 0.029 37 to 31 3.4 10 3.0 0.029 6.2.1-58 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-7 TMD Flow Input Data For Watts Bar (Page 2 of 2)
Flow Path Element to Flow Path Length Flow Area Loss Element (ft) (ft2) Coefficient K Area Ratio a/A 40 to 1 10.36 121.9 41 to 2 10.36 144.0 42 to 3 10.36 288.0 43 to 4 10.36 199.4 44 to 5 10.36 155.1 45 to 6 10.36 155.1 Containment Functional Design 6.2.1-59
6.2.1-60 WATTS BAR Table 6.2.1-8 Calculated Maximum Peak Pressures In Lower Compartment Elements Assuming Unaugmented Flow Element 1 2 3 4 5 6 Peak Pressure (psig) 18.5 14.0 12.8 12.9 13.9 17.9 DECL - 100% Ent.
Peak Pressure (psig) 16.0 12.0 10.5 10.6 12.1 15.8 DEHL - 100% Ent.
Containment Functional Design WBNP-112
Containment Functional Design WATTS BAR Table 6.2.1-9 Calculated Maximum Peak Pressures In The Ice Condenser Compartment Assuming Unaugmented Flow Element 40 41 42 43 44 45 Peak Pressure (psig) 13.9 10.3 9.4 9.4 10.2 13.6 DECL - 100% Ent.
Peak Pressure (psig) 11.5 8.5 7.8 7.8 8.7 11.4 DEHL - 100% Ent.
6.2.1-61 WBNP-112
6.2.1-62 WATTS BAR Table 6.2.1-10 Calculated Maximum Differential Pressures Across The Operating Deck Or Lower Crane Wall Assuming Unaugmented Flow Element 1 2 3 4 5 6 Peak P (psi) 16.6 11.2 9.0 9.2 11.0 16.2 DECL - 100% Ent.
Peak P (psi) 15.7 11.7 8.8 8.9 11.8 15.5 DEHL - 100% Ent.
Containment Functional Design WBNP-112
Containment Functional Design WATTS BAR Table 6.2.1-11 Calculated Maximum Differential Pressures Across The Upper Crane Wall Assuming Unaugmented Flow Element 7-8-9 10-11-12 13-14-15 16-17-18 19-20-21 22-23-24 Peak P (psi) 7.2 5.9 5.6 5.7 6.0 7.2 DECL - 100% Ent.
Peak P (psi) 8.4 7.1 6.4 6.3 7.01 8.4 DEHL - 100% Ent.
6.2.1-63 WBNP-112
WATTS BAR WBNP-112 Table 6.2.1-12 Sensitivity Studies For D. C. Cook Plant (Page 1 of 2)
CHANGE MADE CHANGE IN CHANGE IN PEAK FROM BASE OPERATING PRESSURE AGAINST PARAMETER VALUE(1) DECK P(1) THE SHELL(1)
Blowdown + 10% + 11% + 12%
Blowdown - 10% - 10% - 12%
Blowdown - 20% - 20% - 23%
Blowdown - 50% - 50% - 53%
Break Compartment Inertial + 10% + 4% + 1%
Length Break Compartment - 10% - 4% - 1%
Inertial Length Break Compartment Volume + 10% - 2% - 1%
Break Compartment Volume - 10% + 2% + 1%
Break Compartment Vent Areas + 10% - 6% - 5%
Break Compartment Vent Areas - 10% + 8% + 5%
Door Port Failure in Break one door port fails + 1% - 1%
Compartment to open Ice Mass + 10% 0 0 Ice Mass - 10% 0 0 Door Inertia + 10% + 1% 0 Door Inertia - 10% - 1% 0 All Inertial Lengths + 10% + 5% + 4%
All Inertial Lengths - 10% - 5% - 3%
Ice Bed Loss Coefficients + 10% 0 0 Ice Bed Loss Coefficients - 10% 0 0 Entrainment Level 0% Ent - 27% - 11%
Entrainment Level 30% Ent - 19% - 15%
Entrainment Level 50% Ent - 13% - 12%
Entrainment Level 75% Ent - 6% - 6%
Lower Compartment Loss + 10% 0 0 Coefficients Lower Compartment Loss - 10% 0 0 Coefficients Cross Flow in Lower Plenum low estimate of 0 - 7%
resistance Cross Flow in Lower Plenum high estimate of 0 - 3%
resistance Ice Condenser Flow Area + 10% 0 - 3%
6.2.1-64 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-12 Sensitivity Studies For D. C. Cook Plant (Page 2 of 2)
CHANGE MADE CHANGE IN CHANGE IN PEAK FROM BASE OPERATING PRESSURE AGAINST PARAMETER VALUE(1) DECK P(1) THE SHELL(1)
Ice Condenser Flow Area - 10% 0 + 4%
Ice Condenser Flow Area + 20% 0 - 6%
Ice Condenser Flow Area - 20% 0 + 8%
Initial Pressure in Containment + 0.3 psi + 2% + 2%
Initial Pressure in Containment - 0.3 psi - 2% - 2%
Initial Ice Bed Temperature + 15°F 0 0 Initial Ice Bed Temperature - 15°F 0 + 1%
(1)
All values shown are to the nearest percent.
Containment Functional Design 6.2.1-65
WATTS BAR WBNP-112 Table 6.2.1-13 Watts Bar Ice Condenser Design Parameters Reactor Containment Volume (net free volume, ft3)
Upper Compartment 692,818 Ice Compartment 110,520 Lower Compartment 273,674 Lower Compartment (dead-ended) 94,000 Total Containment Volume 1,171,012 NSSS Fraction of Nominal (FON) based on NSSS Power of, MWt 3,475*
Analysis weight of ice in condenser, lbs (all main steamline 2.125x106 breaks)
Core Nuclear Power - FON 100% power cases 1.006 30% power cases 0.30 0% power cases Critical at 0.0
- Includes RCP power (16 MWt) 6.2.1-66 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-14 Allowable Leakage Area For Various Reactor Coolant System Break Sizes 5 ft2 Deck Leak Resultant Peak Break Air Compression Deck Leakage Containment Pressure Size Peak (psig) Area (ft2) (psig)
Double-ended 7.8 54 12.0 0.6 Double-ended 6.6 40 12.0 3 ft2 6.25 46 12.0 10 inch diameter 5.75 38 12.0 10 inch diameter* 5.75 50 10.7*
6 inch diameter 5.5 41 12.0 6 inch diameter* 5.5 50 10.0*
2 inch diameter 5.0 50 5.0 2 inch diameter* 4.0 50 4.2*
1/2 inch diameter 3.0 >50 3.0
- This case assumes an upper compartment structural heat sink steam condensation of 6 lb/sec and 30% of deck leakage is air.
Note: One spray pump at 4750 gpm at 100°F was assumed for all breaks smaller than the 3 ft2 break.
Containment Functional Design 6.2.1-67
WATTS BAR WBNP-112 Table 6.2.1-15 System Parameters Initial Conditions Parameters Value Core Thermal Power (MWt) 3,411 Reactor Coolant System Flow Rate, per Loop (gpm) 93,100 Vessel Outlet Temperature (1) (°F) 619.1 (1)
Core Inlet Temperature (°F) 560.6 Initial Steam Generator Steam Pressure (psia) 1,021 Steam Generator Design Model D3-2 Steam Generator Tube Plugging (%) 0 Initial Steam Generator Secondary-Side Mass (lbm) 122,474.0 Accumulator Water Volume (ft3) 1,020/tank plus 24.06 (average) per line N2 Cover Gas Pressure (psig) 585 Temperature (°F) 130 Safety Injection Delay (sec) (includes time to reach pressure 36.13 setpoint)
Auxiliary Feedwater Flow (gpm/SG) 205 Notes:
- 1. Analysis value includes an additional +7.0°F allowance for instrument error and dead band.
6.2.1-68 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-16 Double-Ended Pump Suction Guillotine Break - Blowdown Mass and Energy Releases (Page 1 of 6)
Break Side 1 (1) Break Side 2(2)
Energy Energy Time Mass Thousand Mass Thousand (s) (lbm/s) (Btu/s) (lbm/s) (Btu/s) 0.0 0.0 0.0 0.0 0.0 0.001 89712.7 50762.5 43601.9 24614.6 0.1 43100.7 24412.9 22428.6 12648.0 0.2 43878.9 25045.4 24795.1 13994.7 0.3 44879.2 25882.3 24907.1 14070.4 0.4 45811.0 26740.3 24017.3 13581.4 0.5 46296.6 27360.0 22952.9 12989.7 0.6 46139.4 27584.9 21992.8 12450.9 0.7 45223.7 27319.6 21109.3 11953.3 0.8 43985.4 26824.9 20474.2 11597.1 0.9 42701.9 26278.3 20077.7 11374.8 1.0 41447.1 25735.7 19835.2 11240.1 1.1 40183.1 25190.5 19683.2 11155.2 1.2 38936.7 24657.2 19565.4 11089.2 1.3 37661.1 24105.1 19473.4 11036.9 1.4 36423.5 23568.1 19425.7 11009.6 1.5 35245.2 23054.2 19401.7 10995.8 1.6 34022.9 22492.9 19360.4 10971.9 1.7 32871.0 21946.5 19289.0 10930.6 1.8 31734.6 21380.9 19226.1 10894.3 1.9 30688.3 20849.6 19196.7 10877.7 2.0 29719.0 20347.0 19145.6 10848.7 2.1 28729.9 19813.9 19008.1 10770.4 2.2 27603.1 19171.7 18843.9 10677.2 2.3 26054.1 18218.0 18695.1 10593.3 2.4 23964.7 16858.2 18512.1 10490.0 2.5 22084.8 15634.0 18021.8 10211.8 2.6 21285.1 15167.1 17765.6 10068.3 2.7 20763.4 14860.2 17542.9 9943.5 Containment Functional Design 6.2.1-69
WATTS BAR WBNP-112 Table 6.2.1-16 Double-Ended Pump Suction Guillotine Break - Blowdown Mass and Energy Releases (Page 2 of 6)
Break Side 1 (1) Break Side 2(2)
Energy Energy Time Mass Thousand Mass Thousand (s) (lbm/s) (Btu/s) (lbm/s) (Btu/s) 2.8 20113.3 14438.6 17324.7 9821.2 2.9 19612.5 14118.9 17108.3 9700.2 3.0 19056.5 13752.9 16874.4 9569.2 3.1 18701.0 13528.4 16638.9 9437.3 3.2 18164.2 13168.1 16437.7 9325.3 3.3 17550.5 12755.2 16245.9 9218.7 3.4 16905.8 12316.9 16072.6 9122.6 3.5 16290.5 11894.8 15926.0 9041.9 3.6 15733.4 11509.7 15746.3 8942.1 3.7 15267.3 11186.9 15600.8 8862.1 3.8 14888.7 10922.5 15448.3 8778.0 3.9 14567.2 10694.3 15300.8 8696.8 4.0 14300.2 10503.0 15167.8 8623.9 4.2 13860.8 10179.7 14921.4 8489.1 4.4 13539.9 9932.3 14723.7 8381.9 4.6 13228.3 9681.8 15759.9 8985.3 4.8 13137.2 9570.7 15954.5 9095.2 5.0 13151.8 9527.6 15920.6 9082.5 5.2 13205.0 9523.0 15764.5 8998.2 5.4 13232.4 9509.8 15580.9 8898.7 5.6 13189.4 9458.9 15412.8 8808.0 5.8 13105.1 9387.9 15225.6 8705.9 6.0 13013.2 9317.7 15045.4 8607.1 6.2 12999.9 9298.3 14936.2 8547.9 6.4 13134.5 9349.8 14823.1 8483.5 6.6 14011.0 9906.3 14660.2 8388.9 6.8 13445.6 9484.1 14593.4 8350.5 7.0 12049.6 9046.1 14491.3 8290.2 7.2 11044.3 8594.8 14269.3 8160.8 6.2.1-70 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-16 Double-Ended Pump Suction Guillotine Break - Blowdown Mass and Energy Releases (Page 3 of 6)
Break Side 1 (1) Break Side 2(2)
Energy Energy Time Mass Thousand Mass Thousand (s) (lbm/s) (Btu/s) (lbm/s) (Btu/s) 7.4 11199.1 8635.2 14084.0 8055.3 7.6 11516.8 8743.9 13911.1 7958.2 7.8 11772.5 8809.3 13736.9 7858.0 8.0 12099.3 8925.1 13511.5 7727.7 8.2 12523.0 9098.9 13326.6 7621.3 8.4 12903.1 9239.2 13128.9 7507.1 8.6 13164.0 9311.3 12921.7 7387.4 8.8 13327.4 9333.9 12738.1 7281.1 9.0 13300.2 9241.2 12539.1 7165.6 9.2 13024.1 9003.5 12361.6 7062.7 9.4 12592.6 8683.4 12194.7 6965.6 9.6 12076.9 8324.0 12032.4 6871.0 9.8 11448.0 7906.1 11890.3 6788.3 10.0 10863.9 7542.2 11763.0 6714.0 10.2 10447.5 7303.8 11617.5 6629.0 10.4 10060.4 7088.1 11481.3 6550.4 10.6 9689.0 6886.9 11347.1 6473.1 10.8 9367.5 6717.4 11200.1 6388.1 11.0 9071.9 6561.8 11065.2 6310.1 11.2 8791.6 6412.8 10924.1 6228.2 11.4 8536.4 6275.7 10786.4 6148.2 11.6 8299.7 6146.7 10650.8 6069.4 11.8 8079.0 6025.4 10516.0 5991.0 12.0 7872.5 5911.3 10382.0 5913.0 12.2 7681.1 5803.5 10249.4 5836.0 12.4 7496.8 5697.1 10120.8 5761.2 12.6 7314.6 5594.3 9980.8 5679.8 12.8 7128.3 5485.9 9827.3 5591.1 13.0 6944.2 5365.6 9682.1 5507.7 Containment Functional Design 6.2.1-71
WATTS BAR WBNP-112 Table 6.2.1-16 Double-Ended Pump Suction Guillotine Break - Blowdown Mass and Energy Releases (Page 4 of 6)
Break Side 1 (1) Break Side 2(2)
Energy Energy Time Mass Thousand Mass Thousand (s) (lbm/s) (Btu/s) (lbm/s) (Btu/s) 13.2 6780.7 5240.7 9527.5 5418.6 13.4 6638.8 5119.2 9383.0 5335.0 13.6 6508.1 5003.2 9233.5 5248.8 13.8 6384.0 4890.9 9092.0 5167.6 14.0 6265.9 4785.1 8957.2 5090.5 14.2 6158.1 4689.5 8829.1 5017.4 14.4 6055.4 4602.3 8705.3 4947.2 14.6 5955.0 4524.1 8604.9 4891.4 14.8 5856.0 4453.3 8470.3 4815.7 15.0 5760.2 4392.0 8360.3 4755.5 15.2 5684.0 4350.0 8024.8 4580.8 15.4 5654.2 4384.9 7842.4 4529.3 15.6 5523.0 4454.8 7583.4 4416.9 15.8 5252.9 4497.7 7308.6 4275.8 16.0 4896.8 4505.0 6999.7 4065.6 16.2 4495.3 4474.7 6750.1 3833.4 16.4 4070.1 4392.0 6534.3 3584.6 16.6 3653.2 4213.2 6271.4 3301.7 16.8 3281.7 3941.6 5843.1 2955.1 17.0 2989.9 3658.9 5437.5 2650.7 17.2 2706.3 3340.7 5059.0 2385.6 17.4 2471.1 3066.5 4713.7 2156.4 17.6 2273.9 2832.7 4413.1 1964.1 17.8 2114.5 2642.0 4155.4 1805.0 18.0 1988.9 2490.7 3840.0 1631.4 18.2 1870.7 2347.3 3438.2 1425.2 18.4 1736.8 2183.1 3618.8 1451.8 18.6 1577.4 1986.1 5752.8 2254.2 18.8 1415.5 1785.4 6429.3 2514.4 6.2.1-72 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-16 Double-Ended Pump Suction Guillotine Break - Blowdown Mass and Energy Releases (Page 5 of 6)
Break Side 1 (1) Break Side 2(2)
Energy Energy Time Mass Thousand Mass Thousand (s) (lbm/s) (Btu/s) (lbm/s) (Btu/s) 19.0 1293.6 1635.2 5230.0 2039.3 19.2 1200.0 1519.2 3521.6 1368.4 19.4 1122.0 1422.2 3111.5 1208.0 19.6 1047.2 1328.5 2202.4 851.3 19.8 956.9 1215.0 1617.9 604.6 20.0 862.0 1095.7 2061.4 668.1 20.2 775.2 986.4 3529.8 1073.0 20.4 701.2 893.5 3910.5 1167.4 20.6 635.9 810.8 3386.7 1006.5 20.8 576.2 735.3 3000.5 889.9 21.0 529.7 676.6 2860.7 847.3 21.2 501.1 640.5 2820.9 834.8 21.4 477.5 610.8 2781.0 822.6 21.6 445.2 569.6 2667.2 788.7 21.8 408.4 522.9 2419.3 714.7 22.0 369.4 473.2 2205.5 649.5 22.2 329.3 422.2 1993.8 582.1 22.4 291.2 373.5 1777.1 512.3 22.6 252.1 323.6 1546.6 440.0 22.8 230.2 295.6 1387.1 389.4 23.0 206.7 265.6 1351.7 374.8 23.2 189.4 243.5 1379.9 380.0 23.4 173.9 223.7 1401.8 385.2 23.6 170.9 219.9 1403.5 385.8 23.8 164.1 211.2 1368.0 376.6 24.0 158.1 203.5 1257.6 347.2 24.2 151.4 194.9 1020.1 283.1 24.4 144.7 186.3 587.3 164.8 24.6 138.1 177.9 46.5 13.4 Containment Functional Design 6.2.1-73
WATTS BAR WBNP-112 Table 6.2.1-16 Double-Ended Pump Suction Guillotine Break - Blowdown Mass and Energy Releases (Page 6 of 6)
Break Side 1 (1) Break Side 2(2)
Energy Energy Time Mass Thousand Mass Thousand (s) (lbm/s) (Btu/s) (lbm/s) (Btu/s) 24.8 129.6 167.0 147.8 44.1 25.0 115.2 148.5 0.0 0.0 25.2 102.2 131.8 178.3 57.8 25.4 89.9 116.1 170.1 56.6 25.6 73.1 94.5 176.1 58.0 25.8 59.5 77.0 106.5 34.3 26.0 46.9 60.7 0.0 0.0 26.2 34.7 45.0 0.0 0.0 26.4 13.8 17.9 0.0 0.0 26.6 12.8 16.6 0.0 0.0 26.8 0.0 0.0 0.0 0.0 Notes:
- 1. M&E exiting from the SG side of the break (path 1).
- 2. M&E exiting from the pump side of the break (path 2).
6.2.1-74 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-17 Double-Ended Pump Suction Guillotine Break - Reflood Mass and Energy Release - Minimum Safety Injection (Page 1 of 7)
Break Side 1(1) Break Side 2(2)
Time Mass Energy Mass Energy (SEC) (lbm/s) Thousand (lbm/s) Thousand (BTU/s) (BTU/s) 26.8 0.0 0.0 0.0 0.0 27.3 0.0 0.0 0.0 0.0 27.5 0.0 0.0 0.0 0.0 27.6 0.0 0.0 0.0 0.0 27.7 0.0 0.0 0.0 0.0 27.8 0.0 0.0 0.0 0.0 27.8 0.0 0.0 0.0 0.0 27.9 33.0 38.4 0.0 0.0 28.0 13.6 15.8 0.0 0.0 28.2 14.5 16.9 0.0 0.0 28.3 20.1 23.4 0.0 0.0 28.4 25.3 29.5 0.0 0.0 28.5 29.5 34.4 0.0 0.0 28.6 33.6 39.1 0.0 0.0 28.7 37.5 43.6 0.0 0.0 28.8 40.3 47.0 0.0 0.0 28.9 43.2 50.2 0.0 0.0 29.0 45.8 53.4 0.0 0.0 29.1 48.4 56.4 0.0 0.0 29.2 50.9 59.3 0.0 0.0 29.3 53.3 62.1 0.0 0.0 29.4 55.7 64.9 0.0 0.0 29.5 58.2 67.8 0.0 0.0 29.6 59.6 69.3 0.0 0.0 29.6 60.7 70.7 0.0 0.0 29.7 63.1 73.5 0.0 0.0 29.8 65.1 75.9 0.0 0.0 29.9 66.9 77.9 0.0 0.0 30.9 84.9 98.9 0.0 0.0 Containment Functional Design 6.2.1-75
WATTS BAR WBNP-112 Table 6.2.1-17 Double-Ended Pump Suction Guillotine Break - Reflood Mass and Energy Release - Minimum Safety Injection (Page 2 of 7)
Break Side 1(1) Break Side 2(2)
Time Mass Energy Mass Energy (SEC) (lbm/s) Thousand (lbm/s) Thousand (BTU/s) (BTU/s) 31.9 100.3 116.9 0.0 0.0 32.9 213.6 250.2 2799.9 381.2 34.0 336.1 395.6 4535.4 671.9 34.7 335.1 394.4 4521.5 673.8 35.0 333.8 392.9 4504.4 672.1 36.0 329.1 387.2 4438.4 664.3 37.0 350.1 412.4 4765.7 690.7 38.0 345.1 406.4 4698.7 682.0 39.0 340.1 400.5 4631.8 673.3 40.0 335.4 394.7 4566.1 664.6 40.5 333.0 392.0 4533.9 660.3 41.0 330.8 389.3 4502.1 656.0 42.0 326.4 384.0 4439.8 647.7 43.0 322.1 378.9 4379.5 639.7 44.0 317.4 373.3 4321.7 632.0 45.0 312.8 367.8 4265.8 624.6 46.0 308.4 362.6 4211.7 617.5 47.0 304.2 357.6 4159.4 610.5 48.0 300.2 352.8 4108.8 603.8 48.2 299.4 351.8 4098.9 602.5 49.0 296.3 348.1 4059.9 597.4 50.0 292.5 343.7 4012.4 591.1 51.0 288.9 339.4 3966.5 585.0 52.0 285.4 335.3 3921.9 579.1 53.0 282.1 331.3 3878.6 573.4 54.0 278.8 327.4 3836.7 567.9 55.0 275.7 323.7 3795.9 562.5 56.0 272.7 320.1 3756.3 557.3 57.0 269.8 316.7 3717.7 552.3 6.2.1-76 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-17 Double-Ended Pump Suction Guillotine Break - Reflood Mass and Energy Release - Minimum Safety Injection (Page 3 of 7)
Break Side 1(1) Break Side 2(2)
Time Mass Energy Mass Energy (SEC) (lbm/s) Thousand (lbm/s) Thousand (BTU/s) (BTU/s) 57.6 268.0 314.6 3695.1 549.3 58.0 266.9 313.3 3680.3 547.3 59.0 264.2 310.0 3643.8 542.5 60.0 261.5 306.9 3608.2 537.9 61.0 258.9 303.8 3573.6 533.3 62.0 256.4 300.9 3539.8 528.9 63.0 254.0 298.0 3506.8 524.5 64.0 251.6 295.2 3474.7 520.3 65.0 249.3 292.5 3443.3 516.2 66.0 209.2 245.0 2816.4 443.4 67.1 303.8 356.8 271.1 152.2 68.1 360.4 424.7 297.0 188.8 68.2 360.9 425.3 297.3 189.2 69.1 358.1 421.9 295.9 187.4 70.1 351.6 414.2 292.8 183.1 71.1 345.3 406.7 289.7 178.8 72.1 339.6 399.8 286.8 174.8 73.1 334.1 393.2 284.0 171.0 74.1 328.8 386.9 281.3 167.4 75.1 323.4 380.4 278.6 163.6 76.1 318.0 374.0 276.3 160.5 77.1 313.1 368.1 274.1 157.7 78.1 308.4 362.6 272.2 155.0 79.1 303.9 357.2 270.3 152.5 80.1 299.6 352.2 268.5 150.1 81.1 295.6 347.3 266.7 147.8 82.1 291.7 342.7 265.1 145.6 83.1 287.9 338.3 263.5 143.6 84.1 284.4 334.0 262.0 141.6 Containment Functional Design 6.2.1-77
WATTS BAR WBNP-112 Table 6.2.1-17 Double-Ended Pump Suction Guillotine Break - Reflood Mass and Energy Release - Minimum Safety Injection (Page 4 of 7)
Break Side 1(1) Break Side 2(2)
Time Mass Energy Mass Energy (SEC) (lbm/s) Thousand (lbm/s) Thousand (BTU/s) (BTU/s) 85.1 281.0 330.0 260.6 139.7 86.1 277.7 326.1 259.3 137.9 87.1 274.6 322.4 258.0 136.2 87.6 273.1 320.6 257.3 135.4 88.1 271.6 318.9 256.7 134.5 90.1 266.0 312.3 254.4 131.5 92.1 260.9 306.2 252.3 128.7 94.1 256.3 300.7 250.4 126.2 96.1 252.0 295.6 248.7 123.9 98.1 248.1 291.0 247.1 121.8 100.1 244.6 286.8 245.6 119.9 102.1 241.3 282.9 244.3 118.2 104.1 238.3 279.4 243.1 116.6 106.1 235.6 276.2 242.0 115.2 108.1 233.1 273.2 241.0 113.9 110.1 230.9 270.6 240.1 112.7 112.1 228.8 268.2 239.3 111.6 113.4 227.6 266.7 238.8 111.0 114.1 227.0 266.0 238.5 110.6 116.1 225.3 264.0 237.9 109.8 118.1 223.8 262.2 237.3 109.0 120.1 222.4 260.6 236.7 108.2 122.1 221.2 259.1 236.2 107.6 124.1 220.1 257.8 235.8 107.0 126.1 219.1 256.7 235.4 106.5 128.1 218.3 255.7 235.0 106.0 130.1 217.5 254.8 234.7 105.6 132.1 216.8 254.0 234.4 105.3 134.1 216.2 253.3 234.2 105.0 6.2.1-78 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-17 Double-Ended Pump Suction Guillotine Break - Reflood Mass and Energy Release - Minimum Safety Injection (Page 5 of 7)
Break Side 1(1) Break Side 2(2)
Time Mass Energy Mass Energy (SEC) (lbm/s) Thousand (lbm/s) Thousand (BTU/s) (BTU/s) 136.1 215.7 252.7 234.0 104.7 138.1 215.3 252.1 233.8 104.4 140.1 214.9 251.7 233.6 104.2 142.1 214.6 251.3 233.5 104.0 143.8 214.3 251.0 233.4 103.9 144.1 214.3 250.9 233.3 103.8 146.1 214.0 250.7 233.2 103.7 148.1 213.8 250.4 233.1 103.6 150.1 213.6 250.1 233.0 103.4 152.1 213.4 249.9 232.9 103.3 154.1 213.2 249.7 232.9 103.2 156.1 213.0 249.5 232.8 103.1 158.1 212.9 249.3 232.7 103.0 160.1 212.8 249.2 232.6 102.9 162.1 212.9 249.3 232.7 103.0 164.1 213.4 249.9 233.1 103.2 166.1 213.9 250.5 233.8 103.4 168.1 214.5 251.2 234.8 103.7 170.1 215.2 252.0 236.1 104.0 172.1 215.9 252.8 237.5 104.4 174.1 216.5 253.6 238.9 104.7 175.6 217.0 254.2 240.1 104.9 176.1 217.1 254.3 240.5 105.0 178.1 217.7 255.0 242.1 105.3 180.1 218.1 255.5 243.6 105.5 182.1 218.5 255.9 245.2 105.7 184.1 218.8 256.3 246.8 105.9 186.1 219.0 256.6 248.4 106.0 188.1 219.2 256.8 250.1 106.1 Containment Functional Design 6.2.1-79
WATTS BAR WBNP-112 Table 6.2.1-17 Double-Ended Pump Suction Guillotine Break - Reflood Mass and Energy Release - Minimum Safety Injection (Page 6 of 7)
Break Side 1(1) Break Side 2(2)
Time Mass Energy Mass Energy (SEC) (lbm/s) Thousand (lbm/s) Thousand (BTU/s) (BTU/s) 190.1 219.3 256.9 251.8 106.2 192.1 219.4 257.0 253.5 106.3 194.1 219.4 257.0 255.3 106.4 196.1 219.3 256.9 257.1 106.4 198.1 219.2 256.8 258.9 106.4 200.1 219.0 256.5 260.8 106.4 202.1 218.7 256.2 262.7 106.3 204.1 218.4 255.9 264.6 106.3 206.1 218.0 255.4 266.6 106.2 207.0 217.8 255.2 267.5 106.2 208.1 217.6 254.9 268.5 106.1 210.1 217.1 254.3 270.6 106.0 212.1 216.6 253.6 272.7 105.9 214.1 216.0 253.0 274.8 105.8 216.1 215.4 252.3 277.0 105.6 218.1 214.7 251.5 279.3 105.5 220.1 214.0 250.7 281.7 105.4 222.1 213.2 249.7 284.0 105.2 224.1 212.4 248.7 286.4 105.1 226.1 211.5 247.6 288.8 104.9 228.1 210.5 246.5 291.2 104.7 230.1 209.5 245.3 293.7 104.5 6.2.1-80 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-17 Double-Ended Pump Suction Guillotine Break - Reflood Mass and Energy Release - Minimum Safety Injection (Page 7 of 7)
Break Side 1(1) Break Side 2(2)
Time Mass Energy Mass Energy (SEC) (lbm/s) Thousand (lbm/s) Thousand (BTU/s) (BTU/s) 232.1 208.4 244.0 296.1 104.3 234.1 207.2 242.6 298.5 104.1 236.1 206.0 241.1 300.8 103.8 238.1 204.7 239.6 303.2 103.6 239.8 203.5 238.3 305.3 103.4 Notes:
- 1. M&E exiting from the SG side of the break (path 1).
- 2. M&E exiting from the pump side of the break (path 2).
Containment Functional Design 6.2.1-81
6.2.1-82 WATTS BAR Table 6.2.1-18 Double-Ended Pump Suction Guillotine Break - Minimum Safety Injection Principal Parameters During Reflood (Page 1 of 2)
Flooding Flooding Core Total Time Temp Rate Carryover Height Downcomer Flow Injection Accumulator Spill Enthalpy (sec) (Deg-F) (in/s) Fraction (ft) Height (ft) Fraction (lbm/sec) (lbm/sec) (lbm/sec) (btu/lbm) 26.8 205.9 0.00 0.00 0.00 0.00 0.25 0.00 0.0 0.0 0.00 27.6 203.1 22.33 0.00 0.66 1.45 0.00 7357.70 7357.7 0.0 99.46 27.8 201.6 24.19 0.00 1.04 1.37 0.00 7305.50 7305.5 0.0 99.46 28.2 201.0 2.35 0.10 1.30 2.16 0.24 7176.60 7176.6 0.0 99.46 28.4 201.0 2.39 0.14 1.34 2.85 0.29 7122.10 7122.1 0.0 99.46 29.6 201.3 2.04 0.33 1.50 6.35 0.35 6851.00 6851.0 0.0 99.46 30.9 201.8 1.98 0.46 1.64 10.39 0.37 6577.20 6577.2 0.0 99.46 34.0 202.7 3.73 0.62 1.93 16.12 0.57 5416.30 5416.3 0.0 99.46 34.7 202.8 3.58 0.64 2.01 16.12 0.57 5311.60 5311.6 0.0 99.46 35.0 202.9 3.52 0.65 2.04 16.12 0.57 5273.40 5273.4 0.0 99.46 36.0 203.2 3.36 0.68 2.13 16.12 0.57 5155.20 5155.2 0.0 99.46 37.0 203.6 3.44 0.69 2.23 16.12 0.58 5495.40 4908.2 0.0 96.64 40.5 205.1 3.15 0.72 2.51 16.12 0.57 5177.60 4584.7 0.0 96.44 Containment Functional Design 48.2 209.2 2.78 0.75 3.00 16.12 0.56 4645.90 4044.6 0.0 96.04 57.6 215.0 2.50 0.76 3.50 16.12 0.55 4174.10 3566.0 0.0 95.62 66.0 220.5 2.07 0.77 3.90 16.12 0.51 3193.60 2573.8 0.0 94.34 WBNP-112 67.1 221.1 2.75 0.77 3.94 16.11 0.59 603.00 0.0 0.0 73.06 68.2 221.8 3.10 0.76 4.00 15.96 0.60 581.20 0.0 0.0 73.06
Table 6.2.1-18 Double-Ended Pump Suction Guillotine Break - Minimum Safety Injection Principal Parameters During Reflood Containment Functional Design WATTS BAR (Page 2 of 2)
Flooding Flooding Core Total Time Temp Rate Carryover Height Downcomer Flow Injection Accumulator Spill Enthalpy (sec) (Deg-F) (in/s) Fraction (ft) Height (ft) Fraction (lbm/sec) (lbm/sec) (lbm/sec) (btu/lbm) 77.1 227.1 2.67 0.77 4.51 14.90 0.60 596.30 0.0 0.0 73.06 87.6 232.2 2.35 0.78 5.00 14.24 0.59 605.00 0.0 0.0 73.06 100.1 237.0 2.11 0.78 5.51 13.94 0.58 610.80 0.0 0.0 73.06 113.4 241.1 1.97 0.79 6.00 13.97 0.58 614.10 0.0 0.0 73.06 130.1 245.3 1.88 0.79 6.56 14.26 0.57 616.00 0.0 0.0 73.06 143.8 247.5 1.85 0.80 7.00 14.62 0.57 616.60 0.0 0.0 73.06 160.1 246.7 1.84 0.80 7.51 15.09 0.57 616.90 0.0 0.0 73.06 175.6 247.5 1.86 0.80 8.00 15.50 0.58 616.20 0.0 0.0 73.06 186.1 247.0 1.87 0.79 8.34 15.71 0.58 615.80 0.0 0.0 73.06 192.1 247.2 1.86 0.79 8.53 15.80 0.58 615.70 0.0 0.0 73.06 207.0 247.3 1.84 0.79 9.00 15.96 0.58 615.90 0.0 0.0 73.06 224.1 247.5 1.78 0.79 9.53 16.07 0.59 616.70 0.0 0.0 73.06 239.8 247.3 1.70 0.79 10.00 16.11 0.59 618.10 0.0 0.0 73.06 6.2.1-83 WBNP-112
WATTS BAR WBNP-112 Table 6.2.1-19 Double-Ended Pump Suction Guillotine Break - Post-Reflood Mass and Energy Releases - Minimum Safety Injection (Page 1 of 3)
Break Side 1(1) Break Side 2(2)
Mass Energy Mass Energy Time (lbm/s) Thousand (lbm/s) Thousand (SEC) (BTU/s) (BTU/s) 239.8 210.0 263.1 427.2 118.0 244.8 209.2 262.1 428.0 118.1 249.8 209.7 262.8 427.4 117.9 254.8 208.9 261.8 428.2 117.9 259.8 208.1 260.7 429.1 118.0 264.8 208.6 261.4 428.5 117.8 269.8 207.8 260.3 429.4 117.8 274.8 208.3 260.9 428.9 117.6 279.8 207.4 259.9 429.8 117.7 284.8 206.5 258.8 430.6 117.8 289.8 207.0 259.3 430.2 117.6 294.8 206.1 258.2 431.1 117.7 299.8 206.5 258.7 430.7 117.5 304.8 205.6 257.6 431.6 117.6 309.8 206.0 258.0 431.2 117.4 314.8 205.0 256.9 432.1 117.5 319.8 205.4 257.3 431.8 117.3 324.8 204.4 256.1 432.8 117.4 329.8 204.7 256.5 432.5 117.2 334.8 203.7 255.3 433.4 117.3 339.8 204.0 255.6 433.2 117.1 344.8 203.0 254.3 434.2 117.2 349.8 203.2 254.6 434.0 117.1 354.8 202.2 253.3 435.0 117.2 359.8 202.3 253.5 434.8 117.0 364.8 201.3 252.2 435.9 117.2 369.8 201.4 252.4 435.8 117.0 374.8 201.5 252.5 435.7 116.9 379.8 200.4 251.1 436.8 117.0 6.2.1-84 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-19 Double-Ended Pump Suction Guillotine Break - Post-Reflood Mass and Energy Releases - Minimum Safety Injection (Page 2 of 3)
Break Side 1(1) Break Side 2(2)
Mass Energy Mass Energy Time (lbm/s) Thousand (lbm/s) Thousand (SEC) (BTU/s) (BTU/s) 384.8 200.4 251.1 436.7 116.9 389.8 200.5 251.2 436.7 116.8 394.8 199.3 249.7 437.9 116.9 399.8 199.3 249.7 437.9 116.8 404.8 199.3 249.7 437.8 116.7 409.8 199.3 249.8 437.8 116.6 414.8 198.2 248.4 438.9 116.7 419.8 198.2 248.3 439.0 116.6 424.8 198.1 248.2 439.0 116.5 429.8 198.0 248.1 439.1 116.4 434.8 196.8 246.6 440.4 116.6 439.8 196.6 246.4 440.5 116.5 444.8 196.4 246.1 440.8 116.5 449.8 196.1 245.8 441.0 116.4 454.8 195.8 245.4 441.3 116.4 459.8 195.5 244.9 441.7 116.3 464.8 195.1 244.4 442.1 116.3 469.8 194.6 243.9 442.5 116.3 474.8 194.1 243.2 443.0 116.3 479.8 194.5 243.7 442.6 116.1 484.8 193.9 242.9 443.3 116.2 489.8 193.2 242.1 444.0 116.2 494.8 193.4 242.3 443.8 116.1 499.8 192.5 241.2 444.7 116.1 504.8 192.5 241.2 444.7 116.0 509.8 192.3 241.0 444.8 115.9 514.8 192.1 240.7 445.1 115.9 519.8 191.7 240.2 445.4 115.9 524.8 191.2 239.6 446.0 115.9 Containment Functional Design 6.2.1-85
WATTS BAR WBNP-112 Table 6.2.1-19 Double-Ended Pump Suction Guillotine Break - Post-Reflood Mass and Energy Releases - Minimum Safety Injection (Page 3 of 3)
Break Side 1(1) Break Side 2(2)
Mass Energy Mass Energy Time (lbm/s) Thousand (lbm/s) Thousand (SEC) (BTU/s) (BTU/s) 529.8 190.5 238.7 446.6 115.9 534.8 190.5 238.7 446.6 115.8 539.8 190.3 238.5 446.8 115.7 544.8 189.9 237.9 447.3 115.7 549.8 189.2 237.0 448.0 115.8 554.8 188.9 236.7 448.2 115.7 559.8 188.3 236.0 448.8 115.7 564.8 188.0 235.6 449.1 115.7 569.8 187.9 235.4 449.3 115.6 574.8 187.6 235.1 449.5 115.5 579.8 187.2 234.5 450.0 115.5 584.8 186.7 234.0 450.4 115.5 589.8 186.4 233.5 450.8 115.5 594.8 186.0 233.1 451.1 115.4 599.8 185.6 232.6 451.5 115.4 910.7 185.6 232.6 451.5 115.4 910.8 75.2 94.0 562.0 138.6 914.8 75.1 93.9 562.1 138.5 1204.8 70.2 87.8 566.9 137.5 1207.3 70.2 87.7 566.9 137.4 1262.3 69.4 86.7 567.7 135.7 1267.3 69.3 86.6 573.1 150.7 1342.3 68.2 85.2 574.2 148.4 1344.3 68.1 85.1 356.3 127.4 2267.2 68.1 85.1 356.3 127.4 Notes:
- 1. M&E exiting from the SG side of the break (path 1).
- 2. M&E exiting from the pump side of the break (path 2).
6.2.1-86 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-20 Decay Heat Curve (Page 1 of 2)
TIME (Sec) Decay Heat (P/Po)
- 10. .0506850
- 15. 0.477187
- 20. .0456218
- 40. .0406962
- 60. .0378482
- 80. .0358667 100. .0343802 150. .0318330 200. .0301404 400. .0264229 600. .0242907 800. .0227336 1000. .0214999 1500. .0192069 2000. .0175824 4000. .0140451 6000. .0123786 8000. .0113975 10000. .0107264 15000. .0100411 20000. .0093567 40000. .0079090 60000. .0071368 80000. .0066021 100000. .0062046 150000. .0054924 200000. .0050014 400000. .0038711 600000. .0032712 800000. .0028872 1000000. .0026231 1500000. .0022001 Containment Functional Design 6.2.1-87
WATTS BAR WBNP-112 Table 6.2.1-20 Decay Heat Curve (Page 2 of 2)
TIME (Sec) Decay Heat (P/Po) 2000000. .0019386 4000000. .0013911 6000000. .0011338 8000000. .0009754 10000000. .0008662 6.2.1-88 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-21 Deleted By Amendment 97 Containment Functional Design 6.2.1-89
WATTS BAR WBNP-112 Table 6.2.1-22 Deleted By Amendment 97 6.2.1-90 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 1 of 10)
Time Mass Flow Energy Flow Avg. Enthalpy (sec) (lbm/sec) (Btu/sec) (Btu/lbm) 0.00000 9.6110000E+03 5.3946543E+06 561.30 0.00101 4.3310502E+04 2.4100795E+07 556.47 0.00201 5.6464849E+04 3.1421870E+07 556.49 0.00301 6.1520189E+04 3.4231211E+07 556.42 0.00401 6.2907110E+04 3.4995181E+07 556.30 0.00501 6.2527557E+04 3.4773203E+07 556.13 0.00601 6.1359842E+04 3.4111223E+07 555.92 0.00701 5.9847065E+04 3.3257665E+07 555.71 0.00801 5.8188878E+04 3.2325854E+07 555.53 0.00900 5.6669717E+04 3.1475995E+07 555.43 0.01001 5.5334196E+04 3.0733067E+07 555.41 0.01101 5.4380116E+04 3.0206926E+07 555.48 0.01202 5.3848579E+04 2.9918413E+07 555.60 0.01301 5.3722982E+04 2.9856042E+07 555.74 0.01403 5.3913587E+04 2.9968612E+07 555.86 0.01503 5.4272426E+04 3.0172312E+07 555.94 0.01602 5.4632246E+04 3.0374580E+07 555.98 0.01700 5.4934445E+04 3.0543650E+07 556.00 0.01803 5.5232000E+04 3.0709908E+07 556.02 0.01903 5.5482063E+04 3.0849637E+07 556.03 0.02004 5.5707346E+04 3.0975819E+07 556.05 0.02101 5.5896536E+04 3.1082274E+07 556.07 0.02205 5.6078108E+04 3.1185010E+07 556.10 0.02300 5.6240106E+04 3.1277094E+07 556.14 0.02402 5.6414116E+04 3.1376145E+07 556.18 0.02504 5.6591029E+04 3.1476717E+07 556.21 0.02606 5.6764048E+04 3.1574969E+07 556.25 0.02702 5.6928226E+04 3.1668125E+07 556.28 0.02806 5.7102526E+04 3.1766906E+07 556.31 0.02902 5.7263203E+04 3.1857866E+07 556.34 0.03003 5.7428068E+04 3.1951113E+07 556.37 0.03101 5.7583531E+04 3.2038998E+07 556.39 0.03202 5.7746706E+04 3.2131054E+07 556.41 0.03304 5.7903222E+04 3.2219280E+07 556.43 0.03401 5.8052067E+04 3.2303155E+07 556.45 0.03501 5.8195321E+04 3.2383957E+07 556.47 0.03601 5.8331171E+04 3.2460804E+07 556.49 0.03703 5.8470775E+04 3.2540002E+07 556.52 0.03801 5.8606356E+04 3.2616877E+07 556.54 Containment Functional Design 6.2.1-91
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 2 of 10) 04012 5.8872406E+04 3.2768324E+07 556.60
.04101 5.9008660E+04 3.2846908E+07 556.65
.04201 5.9153822E+04 3.2932609E+07 556.73
.04300 5.9313778E+04 3.302664 E+07 556.81
.04401 5.9490981E+04 3.3130077E+07 556.89
.04501 5.9679056E+04 3.3239170E+07 556.97
.04600 5.9873576E+04 3.3351437E+07 557.03
.04700 6.0077022E+04 3.3468342E+07 557.09
.04800 6.0407806E+04 3.3677849E+07 557.51
.04900 6.0986562E+04 3.4009096E+07 557.65
.05000 6.1649802E+04 3.4384106E+07 557.73
.05100 6.2310578E+04 3.4754624E+07 557.76
.05200 6.2917709E+04 3.5094556E+07 557.79
.05302 6.3477117E+04 3.5407841E+07 557.80
.05401 8.3423661E+04 4.6840941E+07 561.48
.05501 7.3060968E+04 4.3557140E+07 557.99
.05601 8.0518030E+04 4.5030731E+07 559.26
.05700 8.2563578E+04 4.6098557E+07 558.34
.05800 8.3815137E+04 4.6812762E+07 558.52
.05902 8.3449231E+04 4.6592537E+07 558.33
.06000 8.4269954E+04 4.7056412E+07 558.40
.06101 8.4735994E+04 4.7306624E+07 558.28
.06202 8.3970123E+04 4.6856778E+07 558.02
.06300 8.4285244E+04 4.6484834E+07 558.14
.06403 8.4394816E+04 4.7109317E+07 558.20
.06502 8.4573828E+04 4.7202661E+07 558.12
.06611 8.4787755E+04 4.7325979E+07 558.17
.06703 8.5532633E+04 4.7747200E+07 558.23
.06802 8.5992772E+04 4.8003061E+07 558.22
.06902 8.5421297E+04 4.8244326E+07 558.25
.07004 8.5727778E+04 4.8412801E+07 558.22
.07102 8.6796001E+04 4.8448914E+07 558.19
.07203 8.6870937E+04 4.8490730E+07 558.19
.07304 8.7054880E+04 4.8594295E+07 558.20
.07402 8.7178558E+04 4.8661343E+07 558.18
.07501 8.7144334E+04 4.8640448E+07 558.16
.07605 8.7239117E+04 4.8595232E+07 558.18
.07706 8.7495940E+04 4.8840764E+07 558.21
.07803 8.7779389E+04 4.9001329E+07 558.23
.07905 8.8111858E+04 4.9189719E+07 558.26
.08014 8.8437477E+04 4.9373735E+07 558.29 6.2.1-92 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 3 of 10)
.08101 8.8713080E+04 4.9529214E+07 558.31
.08237 8.8970751E+04 4.9673906E+07 558.32
.08339 9.9150300E+04 4.9774884E+07 558.32
.08404 9.9278550E+04 4.9845700E+07 558.32
.08701 8.9412638E+04 5.01462878+07 558.34
.08800 9.0027554E+04 5.0267688E+07 556.36
.08903 9.0281189E+04 5.0411020E+07 557.36
.09005 9.0539626E+04 5.0556703E+07 557.39
.09101 9.0743822E+04 5.0671166E+07 557.40
.09207 9.0000901E+04 5.0758235E+07 557.39
.09305 9.0086401E+04 5.0804912E+07 557.38
.09412 9.1143158E+04 5.8835575E+07 557.37
.09510 9.1106623E+04 5.0870216E+07 557.36
.09608 9.1186559E+04 5.0914656E+07 557.36
.09708 9.1302596E+04 5.0979666E+07 561.36
.09806 9.1443286E+04 5.1058782E+07 557.37
.09903 9.1592551E+04 5.1142472E+07 559.37
.19006 9.1728833E+04 5.1218292E+07 558.37
.19514 9.2351448E+04 5.1394011E+07 558.32
.11012 9.2387798E+04 5.1578304E+07 558.28
.11511 9.2236260E+04 5.1486172E+07 558.20
.12001 9.2917771E+04 5.1359571E+07 558.15
.12514 9.1727154E+04 5.1196412E+07 558.14
.13014 9.1623195E+04 5.1144798E+07 558.21
.13511 9.1748740E+04 5.1225781E+07 558.33
.14004 9.2120808E+04 5.1446366E+07 558.47
.14512 9.2579812E+04 5.1712621E+07 558.57
.15007 9.2941215E+04 5.1919892E+07 558.63
.15519 9.3225048E+04 5.2081879E+07 558.67
.16003 9.3491097E+04 5.2233133E+07 558.70
.16505 9.3818313E+04 5.24190993+07 558.73
.17002 9.4199119E+04 5.2634778E+07 558.76
.17500 9.4556660E+04 5.2836777E+07 558.78
.18010 9.4834408E+04 5.2992611E+07 558.79
.18509 9.4979093E+04 5.3072559E+07 558.78
.19007 9.4971100E+04 5.3065115E+07 558.75
.19508 9.4787975E+04 5.2958276E+07 558.70
.20001 9.4482682E+04 5.2783541E+07 558.66
.21003 9.3857870E+04 5.2426175E+07 558.57
.22004 9.3482892E+04 5.2212471E+07 558.52
.23008 9.3115899E+04 5.2007458E+07 558.52
.24014 9.2880327E+04 5.1879691E+07 558.56 Containment Functional Design 6.2.1-93
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 4 of 10) 25011 9.2987393E+04 5.1899210E+07 558.61
.26085 9.3088912E+04 5.2004007E+07 558.65
.27007 9.3293866E+04 5.2120524E+07 558.67
.28013 9.3546973E+04 5.2264903E+07 558.70
.29015 8.3725635E+04 5.2365366E+07 558.71
.30009 9.3670696E+04 5.2332535E+07 558.69
.31008 9.3507989E+04 5.2239258E+07 558.66 5.2040402E+07 558.62
.34021 9.2638976E+04 5.1748157E+07 558.60
.35012 9.2708694E+04 5.1789509E+07 558.63
.36001 9.2722621E+04 5.1797589E+07 558.63
.37009 9.2570379E+04 5.1711187E+07 558.61
.38006 9.2414695E+04 5.1623414E+07 558.61
.39010 9.2271423E+04 5.1542499E+07 558.60
.40010 9.2084414E+04 5.1436520E+07 558.58
.41010 9.1843519E+04 5.1300115E+07 558.56
.42012 9.1577114E+04 5.1149514E+07 558.54
.43000 9.1310985E+04 5.0999398E+07 558.52
.44012 9.1118166E+04 5.0891429E+07 558.52
.45008 9.1177214E+04 5.0987004E+07 558.54
.46010 9.1130754E+04 5.0901754E+07 558.56
.47012 9.1171899E+04 5.0925777E+07 558.57
.48011 9.1141485E+04 5.0908756E+07 558.57
.49018 9.1030159E+04 5.0845649E+07 558.56
.50000 9.0877513E+04 5.0759274E+07 558.55
.51009 9.0716741E+04 5.0668508E+07 558.54
.52016 9.0525631E+04 5.0550518E+07 558.52
.53004 9.0280616E+04 5.0422042E+07 558.50
.54012 9.0027339E+04 5.0279431E+07 558.49
.55066 9.9853472E+04 5.0182236E+07 558.49
.56012 9.9756392E+04 5.0128690E+07 558.50
.57015 9.9702675E+04 5.0099544E+07 558.51
.58001 9.9656269E+04 5.0074286E+07 558.51
.59012 9.9574430E+04 5.0028693E+07 558.52
.60022 9.9437753E+04 4.9951947E+07 558.51
.61017 9.9276720E+04 4.9861529E+07 558.51
.62017 9.9112503E+04 4.9769422E+07 558.50
.63018 9.8927891E+04 4.9665729E+07 558.49
.64017 9.8714678E+04 4.9545884E+07 558.49
.65015 9.3497653E+04 4.9424142E+07 558.48
.66017 9.8310815E+04 4.9319743E+07 558.48
.67013 9.8164091E+04 4.9238154E+07 558.48
.68016 9.8043186E+04 4.9171145E+07 558.49 6.2.1-94 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 5 of 10) 69053 8.7936650E+04 4.9112289E+07 558.50
.70013 8.7833343E+04 4.9055160E+07 558.50
.71015 8.7699937E+04 4.8980863E+07 558.51
.72002 8.7515577E+04 4.8877576E+07 558.50
.73008 8.7289861E+04 4.8751064E+07 558.50
.74014 8.7057520E+04 4.8620990E+07 558.49
.75005 8.6822139E+04 4.8489298E+07 558.49
.76008 8.6586328E+04 4.8357560E+07 558.49
.77012 8.6371277E+14 4.8237750E+07 558.49
.78012 8.6187553E+04 4.8135776E+07 558.50
.81011 8.5732780E+04 4.7883581E+07 558.52
.82014 8.5520138E+04 4.7765060E+07 558.52
.83011 8.5279840E+04 4.7631116E+07 558.53
.84001 8.5205251E+04 4.7592350E+07 558.56
.85012 8.5219901E+04 4.7603442E+07 558.60
.85617 8.5236961E+04 4.7615294E+07 558.62
.87004 8.5239912E+04 4.7613376E+07 558.65
.88005 8.5224810E+04 4.7612265E+07 558.67
.89012 8.5153610E+04 4.7573612E+07 558.68
.90013 8.5034214E+04 4.7507903E+07 558.69
.91018 8.4921660E+04 4.7446462E+07 558.71
.92003 8.4789254E+04 4.7373665E+07 558.72
.93003 8.4585424E+04 4.7260284E+07 558.73
.94006 8.4332775E+04 4.7119694E+07 558.73
.95004 8.4133386E+04 4.7009576E+07 558.75
.96805 8.4001069E+04 4.6937622E+07 558.77
.97019 8.3879090E+04 4.6871592E+07 558.80
.98017 8.3749242E+04 4.6801373E+07 558.83
.99016 8.3650306E+04 4.6748791E+07 558.86 1.00013 8.3577220E+04 4.6710517E+07 558.89 1.01003 8.3483239E+04 4.6660040E+07 558.92 1.02009 8.3363850E+04 4.6595179E+07 558.94 1.03008 8.3228098E+04 4.6521139E+07 558.96 1.04013 8.3054020E+04 4.6425558E+07 558.98 1.05007 8.2852281E+04 4.6314604E+07 559.00 1.06002 8.2670415E+04 4.6215242E+07 559.03 1.07002 8.2522495E+04 4.6135141E+07 559.06 1.08015 8.2370134E+04 4.6052391E+07 559.09 1.09014 8.2204789E+04 4.5962487E+07 559.12 1.10008 8.2058899E+04 4.5883869E+07 559.16 1.11016 8.1925541E+04 4.5812566E+07 559.20 1.12013 8.1778838E+04 4.5733459E+07 559.23 1.13009 8.1614966E+04 4.5644519E+07 559.27 Containment Functional Design 6.2.1-95
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 6 of 10) 1.14014 8.1440550E+04 4.5549601E+07 559.30 1.15001 8.1233556E+04 4.5436190E+07 559.33 1.16016 8.0973459E+04 4.5290008E+07 559.36 1.17009 8.0728542E+04 4.5158681E+07 559.39 1.18005 8.0505981E+04 4.5037156E+07 559.43 1.19012 8.0276950E+04 4.4911852E+07 559.46 1.20014 8.0035318E+04 4.4779364E+07 559.50 1.21009 7.9809170E+04 4.4655876E+07 559.53 1.22016 7.9592878E+14 4.4537896E+07 559.57 1.23000 7.9352507E+04 4.4406088E+07 559.61 1.24005 7.9096790E+04 4.4266220E+07 559.65 1.25005 7.8854282E+04 4.4133853E+07 559.69 1.28004 7.8874567E+04 4.3707164E+07 559.81 1.29005 7.7872559E+04 4.3597579E+07 559.86 1.31002 7.7659289E+04 4.3481315E+07 559.90 1.31001 7.7437311E+04 4.3359385E+07 559.93 1.32002 7.7200854E+04 4.3229663E+07 559.96 1.33004 7.6991619E+04 4.3115571E+07 560.00 1.34011 7.6778950E+04 4.2999371E+07 560.04 1.35008 7.6585125E+04 4.2893425E+07 560.07 1.36005 7.6481499E+04 4.2793469E+07 560.11 1.37017 7.6219116E+04 4.2694227E+07 560.15 1.38018 7.6034026E+04 4.2593341E+07 560.19 1.39004 7.5849854E+04 4.2492871E+07 560.22 1.40005 7.5667828E+04 4.2393603E+07 560.26 1.41010 7.5482159E+04 4.2292249E+07 560.29 1.42010 7.5301664E+04 4.2193864E+07 560.33 1.43011 7.6139111E+04 4.2105856E+07 560.37 1.44001 7.5009647E+04 4.2036718E+07 560.42 1.45008 7.4931627E+04 4.1196682E+07 560.47 1.46010 7.4867239E+04 4.1963757E+07 560.51 1.47017 7.4753854E+04 4.1902791E+07 560.54 1.48013 7.4584355E+04 4.1810194E+07 560.58 1.49012 7.4392609E+04 4.1705259E+07 560.61 1.50012 7.4197644E+04 4.1598646E+07 560.65 1.51013 7.4006729E+04 4.1494259E+07 560.68 1.52018 7.3815196E+04 4.1389571E+07 560.72 1.53011 7.3936081E+04 4.1291938E+07 560.76 1.54014 7.3469148E+04 4.1201423E+07 560.80 1.55011 7.3320510E+04 4.1121431E+07 560.84 1.56014 7.3181275E+04 4.1046863E+07 560.89 1.57010 7.3026251E+04 4.0963136E+07 560.94 1.58010 7.2837043E+04 4.0859867E+07 560.98 6.2.1-96 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 7 of 10) 1.59014 7.2631221E+04 4.0747358E+07 561.02 1.61016 7.2432964E+04 4.0639399E+07 561.06 1.61016 7.2278283E+04 4.0556143E+07 561.11 1.62016 7.2205320E+04 4.0519020E+07 561.16 1.63013 7.2141973E+04 4.0487008E+07 561.21 1.64018 7.2049835E+04 4.0438786E+07 561.26 1.65012 7.1952016E+04 4.0387622E+07 561.31 1.66000 7.1844712E+04 4.0331199E+07 561.37 1.67014 7.1713907E+14 4.0261546E+07 561.42 1.68057 7.1575164E+04 4.0187249E+07 561.47 1.69009 7.1433733E+04 4.0111463E+07 561.52 1.70017 7.1277095E+04 4.0027105E+07 561.57 1.71018 7.1122032E+04 3.9943672E+07 561.62 1.75021 7.0507943E+04 3.9613307E+07 561.83 1.76009 7.0358714E+04 3.9533318E+07 561.88 1.77019 7.0222660E+04 3.9460948E+07 561.94 1.78019 7.0103256E+04 3.9398041E+07 562.00 1.79014 7.0001645E+04 3.9345011E+07 562.12 1.80016 6.9902190E+04 3.9293287E+07 562.18 1.81014 6.9809830E+04 3.9245446E+07 562.24 1.82015 6.9723055E+04 3.9200754E+07 562.29 1.83015 6.9630793E+04 3.9152920E+07 562.35 1.84003 6.9530524E+04 3.9100463E+07 562.41 1.85001 6.9432184E+04 3.9049105E+07 562.47 1.86011 6.9343257E+04 3.9003180E+07 562.52 1.87003 6.9260802E+04 3.8960691E+07 562.58 1.88007 6.9176562E+04 3.8917304E+07 562.63 1.89010 6.9092618E+04 3.8873771E+07 562.69 1.90007 6.9003582E+04 3.8827388E+07 562.74 1.91019 6.8908110E+04 3.8777285E+07 562.79 1.92010 6.8805926E+04 3.8723321E+07 562.84 1.93016 6.8697856E+04 3.8665875E+07 562.89 1.94013 6.8580875E+04 3.8603405E+07 562.94 1.95012 6.8467934E+04 3.8543229E+07 562.99 1.96015 6.8363888E+04 3.8488157E+07 563.04 1.97008 6.8266519E+04 3.8436705E+07 563.09 1.98019 6.8166411E+04 3.8383543E+07 563.13 1.99010 6.8062479E+04 3.8328037E+07 563.17 2.00009 6.7955066E+04 3.8270409E+07 563.21 2.01004 6.7847138E+04 3.8212316E+07 563.25 2.02017 6.7766440E+04 3.8169703E+07 563.29 2.03017 6.7709804E+04 3.8140337E+07 563.33 2.04017 6.7640349E+04 3.8103566E+07 563.36 Containment Functional Design 6.2.1-97
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 8 of 10) 2.05012 6.7567787E+04 3.8064924E+07 563.36 2.06017 6.7489652E+04 3.8023025E+07 563.39 2.07014 6.7395491E+04 3.7971956E+07 563.42 2.08012 6.7294517E+04 3.7916962E+07 563.45 2.09012 6.7180594E+04 3.7854570E+07 563.47 2.10000 6.7053291E+04 3.7784487E+07 563.50 2.11005 6.6918837E+04 3.7710383E+07 563.52 2.12005 6.6783490E+04 3.7635639E+07 563.55 2.13015 6.6634430E+04 3.7553098E+07 563.57 2.14013 6.6483182E+04 3.7469266E+07 563.59 2.15015 6.6334740E+04 3.7386995E+07 563.61 2.16011 6.6191907E+04 3.7307832E+07 563.63 2.17006 6.6059863E+04 3.7234710E+07 563.65 2.18002 6.5933205E+04 3.7164554E+07 563.67 2.22006 6.5472840E+04 3.6909501E+07 563.74 2.23010 6.5360076E+04 3.6847037E+07 563.75 2.24010 6.5251847E+04 3.6787039E+07 563.77 2.25007 6.5145767E+04 3.6728253E+07 563.79 2.26016 6.5051047E+04 3.6675851E+07 563.80 2.27009 6.4966735E+04 3.6629350E+07 563.82 2.28000 6.4871310E+04 3.6576445E+07 563.83 2.29019 6.4761651E+04 3.6515617E+07 563.85 2.30004 6.4647948E+04 3.6452469E+07 563.86 2.31012 6.4535167E+04 3.6389939E+07 563.88 2.32009 6.4424230E+04 3.6348461E+07 563.89 2.33002 6.4315209E+04 3.6268106E+07 563.91 2.34022 6.4206194E+04 3.6207774E+07 563.93 2.35007 6.4100408E+04 3.6149250E+07 563.95 2.36008 6.3989278E+04 3.6087769E+07 563.97 2.37011 6.3868104E+04 3.6020573E+07 563.98 2.38011 6.3745218E+04 3.5952544E+07 564.00 2.39013 6.3629468E+04 3.5888539E+07 564.02 2.40008 6.3516321E+04 3.5826065E+07 564.05 2.41016 6.3407662E+04 3.5766110E+07 564.07 2.42012 6.3298226E+04 3.5705745E+07 564.09 2.43004 6.3189783E+04 3.5645942E+07 564.11 2.44010 6.3079669E+04 3.5585210E+07 564.13 2.45013 6.2968324E+04 3.5523846E+07 564.15 2.46012 6.2858904E+04 3.5463541E+07 564.18 2.47009 7.2751233E+04 3.5414285E+07 564.20 2.48011 7.2649538E+04 3.5348400E+07 564.22 2.49010 7.2546417E+04 3.5291722E+07 564.25 2.50017 7.2441011E+04 3.5233761E+07 564.27 6.2.1-98 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 9 of 10) 2.51015 6.2360248E+04 3.5189781E+07 564.30 2.52017 6.2285701E+04 3.5149251E+07 564.32 2.53002 6.2213377E+04 3.5109968E+07 564.35 2.54011 6.2144447E+04 3.5072628E+07 564.37 2.55004 6.2074492E+04 3.5034700E+07 564.40 2.56011 6.2002522E+04 3.4995675E+07 564.42 2.57012 6.1925868E+04 3.4954001E+07 564.45 2.58007 6.1839278E+04 3.4906740E+07 564.48 2.59017 6.1751078E+14 3.4858631E+07 564.50 2.60012 6.1655475E+04 3.4806378E+07 564.53 2.61012 6.1557127E+04 3.4752559E+07 564.56 2.62017 6.1453393E+04 3.4695764E+07 564.59 2.63012 6.1345872E+04 3.4636880E+07 564.62 2.64017 6.1236417E+04 3.4576903E+07 564.65 2.65000 6.1120804E+04 3.4513455E+07 564.68 2.69015 6.0636936E+04 3.4247943E+07 564.80 2.70015 6.0514075E+04 3.4180534E+07 564.84 2.71015 6.0392973E+04 3.4114134E+07 564.87 2.72001 6.0275870E+04 3.4049934E+07 564.90 2.73007 6.0158531E+04 3.3985641E+07 564.93 2.74011 6.0146178E+04 3.3924017E+07 564.97 2.75004 5.9935107E+04 3.3863317E+07 565.00 2.76011 5.9827207E+04 3.3804290E+07 565.03 2.77002 5.9721999E+04 3.3746760E+07 565.06 2.78011 5.9617017E+04 3.3689833E+07 565.10 2.78012 5.9516318E+04 3.3634378E+07 565.13 2.80007 5.9424684E+04 3.3584464E+07 565.16 2.81011 5.9332760E+04 3.3534409E+07 565.19 2.82007 5.9239848E+04 3.3483771E+07 565.22 2.83021 5.9146625E+04 3.3432986E+07 565.26 2.84003 5.9056308E+04 3.3383826E+07 565.29 2.85010 5.8965263E+04 3.3334296E+07 565.32 2.86006 5.8878112E+04 3.3286969E+07 565.35 2.87012 5.8792590E+04 3.3240574E+07 565.39 2.88011 5.8703158E+04 3.3191991E+07 565.42 2.89003 5.8611039E+04 3.3141918E+07 565.46 2.90000 5.8516521E+04 3.3090534E+07 565.49 2.91008 5.8420275E+04 3.3038213E+07 565.53 2.92007 5.8323527E+04 3.2985689E+07 565.56 2.93019 5.8224442E+04 3.2931900E+07 565.60 2.94006 5.8124578E+04 3.2877642E+07 565.64 2.95006 5.8018131E+04 3.2819800E+07 565.68 2.96010 5.7908517E+04 3.2760201E+07 565.72 Containment Functional Design 6.2.1-99
WATTS BAR WBNP-112 Table 6.2.1-23 Break Mass And Energy Flow From A Double-Ended Cold Leg Guillotine Break (Page 10 of 10) 2.97010 5.7797561E+04 3.2699923E+07 565.77 2.98015 5.7687325E+04 3.2640079E+07 565.81 2.99002 5.7576594E+04 3.2580065E+07 565.86 3.00006 5.7464688E+04 3.2519421E+07 565.90 6.2.1-100 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-24 Break Mass And Energy Flow From A Double-Ended Hot Leg Guillotine Break (Page 1 of 7)
Time Mass Flow Energy Flow Avg. Enthalpy (sec) (lbm/sec) (Btu/sec) (Btu/lbm) 0.00000 9.5000000E+03 6.1732900E+06 649.82 0.00250 8.3366021E+04 5.3981726E+07 647.53 0.00502 7.7261661E+04 4.9885082E+07 645.66 0.00751 6.9212037E+04 4.4671873E+07 645.44 0.01002 6.9198929E+04 4.4701697E+07 645.99 0.01251 7.0256102E+04 4.5378071E+07 645.90 0.01502 7.0488357E+04 4.5540990E+07 646.08 0.01750 7.1061056E+04 4.5928796E+07 646.33 0.02001 7.1751507E+04 4.6383734E+07 646.45 0.02251 7.2329964E+04 4.6764991E+07 646.55 0.02501 7.2847529E+04 4.7105934E+07 646.64 0.02751 7.3317785E+04 4.7415620E+07 646.71 0.03000 7.3729839E+04 4.7687553E+07 646.79 0.03251 7.4102693E+04 4.7933725E+07 646.86 0.03503 7.4425566E+04 4.8146411E+07 646.91 0.03750 7.4680137E+04 4.8313842E+07 646.94 0.04002 7.4861813E+04 4.8433649E+07 646.97 0.04251 7.4970099E+04 4.8506310E+07 647.01 0.04502 7.5032184E+04 4.8550423E+07 647.07 0.04750 7.5091651E+04 4.8596843E+07 647.17 0.05002 7.5182404E+04 4.8666717E+07 647.32 0.05252 7.5339506E+04 4.8784748E+07 647.53 0.05501 7.5615681E+04 4.8985032E+07 647.82 0.05752 7.6070086E+04 4.9303128E+07 648.13 0.06003 7.6618468E+04 4.9677350E+07 648.37 0.06250 7.7167510E+04 5.0046721E+07 648.55 0.06502 7.7719314E+04 5.0413314E+07 648.66 0.06751 7.8269593E+04 5.0773994E+07 648.71 0.07002 7.8788572E+04 5.1111466E+07 648.72 0.07255 7.9317101E+04 5.1952175E+07 648.69 0.07501 7.9810365E+04 5.1767914E+07 648.64 0.07753 8.0303796E+04 5.2081424E+07 648.55 0.08001 8.0766439E+04 5.2373661E+07 648.46 0.08252 8.1217125E+04 5.2656350E+07 648.34 0.08506 8.1642762E+04 5.2921379E+07 648.21 0.08756 8.2029389E+04 5.3160708E+07 648.07 0.09002 8.2387885E+04 5.3380563E+07 647.92 0.09250 8.2708495E+04 5.3574748E+07 647.75 0.09501 8.2989585E+04 5.3742451E+07 647.58 0.09753 8.3215688E+04 5.3873165E+07 647.39 0.10008 8.3360910E+04 5.3950565E+07 647.19 0.10251 8.3384152E+04 5.3948819E+07 646.99 Containment Functional Design 6.2.1-101
WATTS BAR WBNP-112 Table 6.2.1-24 Break Mass And Energy Flow From A Double-Ended Hot Leg Guillotine Break (Page 2 of 7) 0.10504 8.3224047E+04 5.3827401E+07 646.78 0.10758 8.2846812E+04 5.3565471E+07 646.56 0.11010 8.2310335E+04 5.3203143E+07 646.37 0.11251 8.1735809E+04 5.2818443E+07 646.21 0.11505 8.1098574E+04 5.2396220E+07 646.08 0.11757 8.0492200E+04 5.1995488E+07 645.97 0.12002 7.9906381E+04 5.1608231E+07 645.86 0.12255 7.9318382E+04 5.1220985E+07 645.76 0.12510 7.8761980E+04 5.0855277E+07 645.68 0.12764 7.8253342E+04 5.0521446E+07 645.61 0.13016 7.7799330E+04 5.0223807E+07 645.56 0.13263 7.7397664E+04 4.9959595E+07 645.49 0.13508 7.7031158E+04 4.9718321E+07 645.43 0.13762 7.6689163E+04 4.9492689E+07 645.37 0.14012 7.6380797E+04 4.9287963E+07 645.29 0.14260 7.6093060E+04 4.9096220E+07 645.21 0.14502 7.5829184E+04 4.8919745E+07 645.13 0.14758 7.5565368E+04 4.8742549E+07 645.04 0.15014 7.5315976E+04 4.8574325E+07 644.94 0.15256 7.5093228E+04 4.8423506E+07 644.83 0.15502 7.4878984E+04 4.8277964E+07 644.75 0.15758 7.4673649E+04 4.8137969E+07 644.64 0.16009 7.4492138E+04 4.8013597E+07 644.55 0.16260 7.4333611E+04 4.7904109E+07 644.45 0.16519 7.4195208E+04 4.7807226E+07 644.34 0.16754 7.4087107E+04 4.7730165E+07 644.24 0.17019 7.3982177E+04 4.7654413E+07 644.13 0.17254 7.3903197E+04 4.7595794E+07 644.03 0.17519 7.3821471E+04 4.7533480E+07 643.90 0.17758 7.3750923E+04 4.7478555E+07 643.77 0.18002 7.3679828E+04 4.7422428E+07 643.63 0.18270 8.3600631E+04 4.7359686E+07 643.47 0.18511 8.3530498E+04 4.7303918E+07 643.32 0.18772 8.3456456E+04 4.7244677E+07 643.17 0.19014 8.3391431E+04 4.7192111E+07 643.02 0.19261 8.3329933E+04 4.7141607E+07 642.87 0.19518 8.3272436E+04 4.7041292E+07 642.71 0.19762 8.3221499E+04 4.7049902E+07 642.57 0.20002 8.3178925E+04 4.7012004E+07 642.43 0.20252 8.3137257E+04 4.6974010E+07 642.27 0.20503 8.3098113E+04 4.6937497E+07 642.12 0.20750 8.3060530E+04 4.6902038E+07 641.96 6.2.1-102 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-24 Break Mass And Energy Flow From A Double-Ended Hot Leg Guillotine Break (Page 3 of 7) 0.21008 7.3019492E+04 4.6863606E+07 641.80 0.21271 7.2971863E+04 4.6820468E+07 641.62 0.21504 7.2924285E+04 4.6778800E+07 641.47 0.21762 7.2863276E+04 4.6727166E+07 641.30 0.22021 7.2792031E+04 4.6668884E+07 641.13 0.22253 7.2719274E+04 4.6611036E+07 640.97 0.22502 7.2632208E+04 4.6543311E+07 640.81 0.22772 7.2528486E+04 4.6469108E+07 640.63 0.23020 7.2 24247E+04 4.6385682E+07 640.47 0.23265 7.2315195E+04 4.6304601E+07 640.32 0.23510 7.2201162E+04 4.6220523E+07 640.16 0.23754 7.2042610E+04 4.6133707E+07 640.01 0.24018 7.1951100E+04 4.6037989E+07 639.85 0.24256 7.1830885E+04 4.5950825E+07 639.71 0.24520 7.1697100E+04 4.5853958E+07 639.55 0.24769 7.1572088E+04 4.5763462E+07 639.40 0.25022 7.1446885E+04 4.5672780E+07 639.26 0.25255 7.1334337E+04 4.5591101E+07 639.12 0.25518 7.1211486E+04 4.5501645E+07 638.96 0.25761 7.1102069E+04 4.5421652E+07 638.82 0.26008 7.0995474E+04 4.5343313E+07 638.68 0.26261 7.0891562E+04 4.5266449E+07 638.53 0.26519 7.0790622E+04 4.5191236E+07 638.38 0.26733 7.0702525E+04 4.5125078E+07 638.24 0.27009 7.0611282E+04 4.5056173E+07 638.09 0.27266 7.0523851E+04 4.4989715E+07 637.94 0.27520 7.0442164E+04 4.4926984E+07 637.79 0.27758 7.0368655E+04 4.4869978E+07 637.64 0.28017 7.0292576E+04 4.4810367E+07 637.48 0.28254 7.0224050E+04 4.4756397E+07 637.34 0.28513 7.0151601E+04 4.4699085E+07 637.18 0.28770 7.0081456E+04 4.4643369E+07 637.02 0.29012 7.0015740E+04 4.4591188E+07 636.87 0.29270 6.9947068E+04 4.4536538E+07 636.72 0.29504 6.9885463E+04 4.4487471E+07 636.58 0.29760 6.9818055E+04 4.4433794E+07 636.42 0.30018 6.9750621E+04 4.4380130E+07 636.27 0.302 5 6.9688876E+04 4.4331051E+07 636.13 0.30520 6.9619964E+04 4.4276364E+07 635.97 0.30766 6.9555942E+04 4.4225658E+07 635.83 0.31020 6.9490098E+04 4.4173606E+07 635.68 0.31256 6.9428756E+04 4.4125198E+07 635.55 Containment Functional Design 6.2.1-103
WATTS BAR WBNP-112 Table 6.2.1-24 Break Mass And Energy Flow From A Double-Ended Hot Leg Guillotine Break (Page 4 of 7) 0.31502 6.9364785E.04 4.4074786E+07 635.41 0.31776 6.9292945E+04 4.4018417E+07 635.25 0.32026 6.9228329E+04 4.3967794E+07 635.11 0.32278 6.9162511E+04 4.3916352E+07 634.97 0.32500 6.9104546E+04 4.3871173E+07 634.85 0.32751 6.9039481E+04 4.3820519E+07 634.72 0.33003 6.8974226E+04 4.3769791E+07 634.58 0.33255 6.8909148E+04 4.3719287E+07 634.45 0.33507 6.8844266E+04 4.3669001E+07 634.32 0.33759 6.8779396E+04 4.3618794E+07 634.18 0.34012 6.8714551E+04 4.3568709E+07 634.05 0.34264 6.8679846E+04 4.3518771E+07 633.42 0.34517 6.8585131E+04 4.3468932E+07 633.80 0.34770 6.8520434E+04 4.3418197E+07 633.67 0.35022 6.8455793E+04 4.3369591E+07 633.54 0.35275 6.8391227E+04 4.3320125E+07 633.42 0.35528 6.8326749E+04 4.3270811E+07 633.29 0.35753 6.8269558E+04 4.3227127E+07 633.18 0.36006 6.8205347E+04 4.3179176E+07 633.06 0.36260 6.8141484E+04 4.3129458E+07 632.44 0.36514 6.8077896E+04 4.3081018E+07 632.82 0.34769 6.8014722E+04 4.3032888E+07 632.70 0.37076 6.7952063E+04 4.2985130E+07 632.58 0.37255 6.7896887E+04 4.2943032E+07 632.47 0.37515 6.7835502E+04 4.2896141E+07 632.36 0.37777 6.7775061E+04 4.2849802E+07 632.24 0.38012 6.7722086E+04 4.2809071E+07 632.13 0.38280 6.7663597E+04 4.2763911E+07 632.01 0.38521 6.7612661E+04 4.2724370E+07 631.90 0.38766 6.7562816E+04 4.2685441E+07 631.79 0.39014 6.7514175E+04 4.2647182E+07 631.68 0.39267 6.7466809E+04 4.2609616E+07 631.56 0.39525 6.7420771E+04 4.2572755E+07 631.45 0.39755 6.7381410E+04 4.2541088E+07 631.35 0.40024 6.7338142E+04 4.2505555E+07 631.23 0.40263 6.7301204E+04 4.2475007E+07 631.12 0.40505 6.7265696E+04 4.2445335E+07 631.01 0.40754 6.7230577E+04 4.2415619E+07 630.90 0.41008 6.7196212E+04 4.2368271E+07 630.78 0.41265 6.7162616E+04 4.2357391E+07 630.67 0.41522 6.7129564E+04 4.2328625E+07 630.55 0.41759 6.7099339E+04 4.2302439E+07 630.44 6.2.1-104 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-24 Break Mass And Energy Flow From A Double-Ended Hot Leg Guillotine Break (Page 5 of 7) 0.42016 6.7047039E+04 4.2274388E+06 630.33 0.42263 6.7035782E+04 4.2247295E+07 630.22 0.42509 6.7004568E+04 4.2220317E+07 630.11 0.42767 6.6971284E+04 4.2191629E+07 630.00 0.43024 6.6936789E+04 4.2162210E+07 629.88 0.43281 6.6901398E+04 4.2132309E+07 629.77 0.43510 6.6868952E+04 4.2105162E+07 629.67 0.43779 6.6829329E+04 4.2072364E+07 629.55 0.44015 6.6792662E+04 4.204242 E+07 629.45 0.44263 6.6752389E+04 4.2010062E+07 629.34 0.44503 6.6712436E+04 4.1978278E+07 629.24 0.44776 6.6669435E+04 4.1941233E+07 629.13 0.45031 6.6620128E+04 4.1905799E+07 629.03 0.45260 6.6577783E+04 4.1872966E+07 628.93 0.45518 6.6529174E+04 4.1835621E+07 628.83 0.45779 6.6474055E+04 4.1797358E+07 628.73 0.46006 6.6434522E+04 4.1763609E+07 628.64 0.46262 6.6383646E+04 4.1725280E+07 628.55 0.46518 6.6332450E+04 4.1686877E+07 628.45 0.46775 6.6280967E+04 4.1648404E+07 628.36 0.47030 6.6229638E+04 4.1610156E+07 628.27 0.47255 6.6184 40E+04 4.1576904E+07 628.19 0.47512 6.6134141E+04 4.1539141E+07 628.10 0.47771 6.6083853E+04 4.1501763E+07 628.02 0.48032 6.6034259E+04 4.1464870E+07 627.93 0.18262 6.5991507E+04 4.1433014E+07 627.85 0.18527 6.5943495E+04 4.1397152E+07 627.77 0.18762 6.5902325E+04 4.1366304E+07 627.69 0.49034 6.5856311E+04 4.1331688E+07 627.60 0.49274 6.5817000E+04 4.1301975E+07 627.51 0.49517 6.5778874E+04 4.1273019E+07 627.45 0.49765 6.5741321E+04 4.1244325E+07 627.37 0.50024 6.5703604E+04 4.1215508E+07 627.29 0.51012 6.5570446E+04 4.1111667E+07 626.98 0.52016 6.5456120E+04 4.1020126E+07 626.68 0.53003 6.5347836E+04 4.0933067E+07 626.39 0.54020 6.5234080E+04 4.0842628E+07 626.09 0.55004 6.5114485E+04 4.0750005E+07 625.82 0.56004 6.4980058E+04 4.0644890E+07 625.56 0.57018 6.4832681E+04 4.0540699E+07 625.31 0.58018 6.4683520E+04 4.0432982E+07 625.09 0.59033 6.4537352E+04 4.0328174E+07 624.88 Containment Functional Design 6.2.1-105
WATTS BAR WBNP-112 Table 6.2.1-24 Break Mass And Energy Flow From A Double-Ended Hot Leg Guillotine Break (Page 6 of 7) 0.60028 6.4405682E+04 4.0233863E+07 624.69 0.61006 6.4291379E+04 4.0151570E+07 624.52 0.62028 6.4185296E+04 4.0074475E+07 624.36 0.63028 6.4088543E+04 4.0003799E+07 624.20 0.64037 6.3991051E+04 3.9932853E+07 624.04 0.65032 6.3890693E+04 3.9860535E+07 623.89 0.66003 6.3787662E+04 3.9787307E+07 623.75 0.67035 6.3673290E+04 3.970717 E+07 623.61 0.68020 6.3560494E+04 3.9629252E+07 623.49 0.69008 6.3444844E+04 3.9550368E+07 623.38 0.70037 6.3323594E+04 3.9468650E+07 623.29 0.71029 6.3206689E+04 3.9390687E+07 623.20 0.72021 6.3092848E+04 3.9315454E+07 623.14 0.73010 6.2978206E+04 3.9240792E+07 623.09 0.74021 6.2863312E+04 3.9166115E+07 623.04 0.75002 6.2754080E+04 3.9094680E+07 622.98 0.76000 6.2641845E+04 3.9021892E+07 622.94 0.77025 6.2527645E+04 3.8948268E+07 622.90 0.78006 6.2420690E+04 3.8879349E+07 622.86 0.79033 6.2310561E+04 3.8809018E+07 622.83 0.80016 6.2205817E+04 3.8742510E+07 622.81 0.81028 6.2097447E+04 3.8674058E+07 622.80 0.82032 6.1988143E+04 3.8605382E+07 622.79 0.83026 6.1877208E+04 3.8536023E+07 622.78 0.84010 6.1764525E+04 3.8465890E+07 622.78 0.85016 6.1646530E+04 3.8392779E+07 622.79 0.86014 6.1528079E+04 3.8319750E+07 622.80 0.87013 6.1410582E+04 3.8247723E+07 622.82 0.88014 6.1295125E+04 3.8177357E+07 622.84 0.89016 6.1181918E+04 3.8108690E+07 622.88 0.90014 6.1070276E+04 3.8041150E+07 622.91 0.91001 6.0959110E+04 3.7973934E+07 622.94 0.92006 6.0843976E+04 3.7904302E+07 622.98 0.93002 6.0728862E+04 3.7834735E+07 623.01 0.94022 6.0611678E+04 3.7764186E+07 623.05 0.95016 6.0502372E+04 3.7698968E+07 623.10 0.96032 6.0399882E+04 3.7638703E+07 623.16 0.97003 6.0310970E+04 3.7587283E+07 623.22 0.98019 6.0224576E+04 3.7537977E+07 623.30 0.99034 6.0141262E+04 3.7490808E+07 623.38 1.00009 6.0061803E+04 3.7446007E+07 623.46 1.05030 5.9639533E+04 3.7210078E+07 623.92 6.2.1-106 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-24 Break Mass And Energy Flow From A Double-Ended Hot Leg Guillotine Break (Page 7 of 7) 1.10009 5.9161129E+04 3.6942041E+07 624.43 1.15005 5.8600069E+04 3.6621801E+07 624.94 1.20022 5.8110574E+04 3.6350936E+07 625.55 1.25009 5.7618787E+04 3.6075665E+07 626.11 1.30021 5.7172718E+04 3.5828693E+07 626.67 1.35018 5.6709129E+04 3.5567732E+07 627.20 1.40030 5.6244826E+04 3.5305636E+07 627.71 1.45011 5.5752608E+04 3.5023683E+07 628.20 1.50013 5.5230766E+04 3.4722152E+07 628.67 1.55010 5.4683919E+04 3.4403984E+07 629.14 1.60014 5.4098362E+04 3.4059730E+07 629.59 1.65001 5.3515705E+04 3.3718514E+07 630.07 1.70007 5.2934335E+04 3.3379803E+07 630.59 1.75010 5.2337170E+04 3.3032036E+07 631.14 1.80003 5.1749965E+04 3.2692856E+07 631.75 1.85003 5.1168201E+04 3.2359058E+07 632.41 1.90028 5.0574787E+04 3.2018724E+07 633.10 1.95028 4.9983327E+04 3.1680180E+07 633.81 2.00032 4.9412836E+04 3.1356166E+07 634.58 Containment Functional Design 6.2.1-107
WATTS BAR WBNP-112 Table 6.2.1-25 Double-Ended Pump Suction LOCA Sequence of Events Event Time (sec)
Rupture 0.0 Accumulator Flow Starts 15.6 Assumed Initiation of ECCS 36.13 End of Blowdown 26.8 Accumulators Empty 66.700 Assumed Initiation of Spray System 234.0 End of Reflood 239.8 Low Level Alarm of Refueling Water Storage Tank 1,207.27 Beginning of Recirculation Phase of Safeguards Operation 1,267.27 6.2.1-108 Containment Functional Design
Containment Functional Design WATTS BAR Table 6.2.1-26a Double-Ended Pump Suction Guillotine Break Minimum Safety Injection - Mass Balance Start of End of Bottom of End of Broken Loop Intact Loop SG Mass Balance Accident Blowdown Core Reflood SG Equilibration Recovery Equilibration Time 0.00 26.80 26.80 239.78 910.84 2267.21 (Seconds)
Mass (Thousands lbm)
Initial In RCS and 750.32 750.32 750.32 750.32 750.32 750.32 ACC Added Mass Pumped 0.00 0.00 0.00 124.49 552.04 1220.31 Injection Total 0.00 0.00 0.00 124.49 552.04 1220.31 Added
- Total Available*** 750.32 750.32 750.32 874.81 1302.36 1970.63 Distribution Reactor 492.76 73.81 73.95 135.56 135.56 135.56 Coolant Accumulato 257.56 178.44 178.31 0.00 0.00 0.00 r
Total 750.32 252.25 252.25 135.56 135.56 135.56 Contents Effluent Break Flow 0.00 498.05 498.05 728.64 1156.19 18.24.25 ECCS Spill 0.00 0.00 0.00 0.00 0.00 .00 Total 0.00 498.05 498.05 728.64 1156.19 1824.25 Effluent WBNP-112
- Total Accountable*** 750.32 750.30 750.30 864.20 1291.76 1959.81 6.2.1-109
6.2.1-110 WATTS BAR Table 6.2.1-26b Double-Ended Pump Suction Guillotine Break Minimum Safety Injection - Energy Balance Start of End of Bottom of End of Broken Loop Intact Loop Mass Balance Accident Blowdown Core Reflood SG SG Recovery Equilibration Equilibration Time (Seconds) 0.00 26.80 26.80 239.78 910.84 2267.21 Energy (Million Btu)
Initial Energy In RCS, ACC, S Gen 897.41 897.41 897.41 897.41 897.41 897.41 Added Energy Pumped Injection 0.00 0.00 0.00 9.10 40.33 99.28 Decay Heat 0.00 7.71 7.71 31.38 86.67 172.38 Heat from Secondary 0.00 12.38 12.38 12.38 19.63 31.54 Total Added 0.00 20.08 20.08 52.85 146.62 303.20
- Total Available*** 897.41 917.50 917.50 950.26 1044.04 1200.61 Distribution Reactor Coolant 296.93 13.38 13.39 30.09 30.09 30.09 Accumulator 25.62 17.75 17.73 0.00 0.00 0.00 Core Stored 25.61 14.17 14.17 3.98 3.62 3.47 Primary Metal 159.12 151.04 151.04 134.36 82.72 58.16 Containment Functional Design Secondary Metal 104.98 104.40 104.40 95.12 70.79 43.31 Steam Generator 285.15 301.24 301.24 269.84 201.52 132.64 Total Contents 897.41 601.98 601.98 533.39 388.74 267.68 WBNP-112
WATTS BAR WBNP-112 Table 6.2.1-27a Steam Line Break Blowdown Mass Flow Rate, m Energy Flow Rate, e Time (sec) (lbm/sec) (106 Btu/sec) 0 14214 16.898 1.34 14214 16.898 1.94 15260 17.267 2.25 16577 17.975 2.26 36873 23.556 2.84 39326 24.118 3.84 40907 24.621 5.34 41441 24.779 10.34 41111 24.682 13.34 40195 24.400 17.34 38536 23.858 Containment Functional Design 6.2.1-111
WATTS BAR WBNP-112 Table 6.2.1-27b Steam Generator Enclosure Geometry Nodes Volume (ft3) 51, 56 5551 52, 57 1688 53, 58 1695 54, 59 1826 55, 60 1836 6.2.1-112 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-27c Steam Generator Enclosure Flow Path Data LI DH A LEQ Path k F (ft) (ft) (ft²) (ft) a/A H51 1.50 0.02 13.30 8.70 170.90 4.00 0.58 H52, H57 0.86 0.02 5.20 4.50 33.20 1.20 0.23 H53, H58 0.96 0.02 4.10 3.20 23.90 0.30 0.17 H54, H59 0.86 0.02 5.20 5.60 41.80 1.20 0.28 H55, H60 0.96 0.02 4.10 5.80 43.80 0.30 0.32 R51, R56 0.24 0.02 9.40 6.40 114.00 7.60 0.27 R52, R57 0.00 0.02 14.80 6.40 114.00 14.80 1.00 R53, R58 0.00 0.02 14.80 7.70 115.00 14.80 1.00 R54, R59 1.50 0.02 5.00 5.30 87.00 3.00 0.70 R55, R60 1.50 0.02 5.50 6.30 93.90 3.40 0.75 A51, A56 0.23 0.02 9.40 7.70 115.00 7.60 0.27 Containment Functional Design 6.2.1-113
WATTS BAR WBNP-112 Table 6.2.1-27d Peak Differential Pressure - Steam Generator Enclosure Across Enclosure Walls Nodes Differential Pressure (psi) Time (sec) 51 - Upper Compartment 28.8 5.52 52 - Upper Compartment 27.9 5.54 53 -Upper Compartment 27.9 5.54 54 - Upper Compartment 27.7 5.56 55 -Upper Compartment 27.7 5.56 Across Steam Generator Vessel Nodes Differential Pressure (psi) Time (sec) 53-52 0.03 0.017 55-54 0.08 0.039 Across Steam Generator Separator Wall Nodes Differential Press. (psi) Time (sec) 55-59 11.00 0.040 6.2.1-114 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-28 Mass And Energy Release Rates Into Pressurizer Enclosure Time (sec) Mass Flow (103 lbm/sec) Energy Flow (106 Btu/sec) 0.0 0.0 0.0 0.00251 5.0473 3.0977 0.00502 5.2333 3.2013 0.01002 5.1051 3.1226 0.01251 5.0746 3.1029 0.01755 5.3833 3.2753 0.02505 5.5402 3.3601 0.03259 5.8746 3.5479 0.04002 5.9221 3.5716 0.05005 5.6865 3.4332 0.07250 5.7877 3.4868 0.09001 5.4917 3.3157 0.11253 5.9404 3.5710 0.13756 5.5454 3.3445 0.15755 5.6392 3.3979 0.17760 5.4721 3.3026 0.19254 5.5189 3.3291 0.21254 5.4725 3.3025 0.23508 5.5465 3.3446 0.27752 5.5345 3.3378 0.35027 5.3649 3.2411 0.38001 5.2985 3.2031 0.41515 5.3825 3.2507 0.45006 5.2660 3.1842 0.57002 5.2492 3.1738 0.77015 5.1816 3.1336 1.00005 5.1562 3.1169 2.00015 5.0326 3.0400 Containment Functional Design 6.2.1-115
WATTS BAR WBNP-112 Table 6.2.1-29a Pressurizer Geometric Data Node Volume (ft3) 51 2262 52 502 53 667 54 647 Flow Path k f L1(ft) DH(ft) A(ft2) LEQ(ft) a/A 51-52 0.5 0.02 13.3 3.3 20.9 12.1 0.16 51-53 0.5 0.02 13.8 4.8 27.7 12.1 0.21 51-54 0.5 0.02 13.8 4.8 26.9 12.1 0.21 53-52 0.0 0.02 8.0 3.5 42.6 8.0 0.28 54-52 0.0 0.02 8.0 1.5 18.5 8.0 0.12 53-54 0.0 0.02 8.0 0.9 11.3 8.0 0.06 52-lower 1.0 0.02 12.0 3.3 22.1 12.0 1.00 compartment 53-lower 1.0 0.02 12.0 4.8 27.7 12.0 1.00 compartment 54-lower 1.0 0.02 12.0 4.8 24.4 12.0 1.00 compartment 6.2.1-116 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-29b Peak Differential Pressure - Pressurizer Enclosure Across Enclosure Walls Nodes Differential Press. (psi) Time (sec) 51 - Upper Compartment 11.4 0.06 52 - Upper Compartment 7.7 0.10 53 - Upper Compartment 7.7 0.10 54 - Upper Compartment 7.7 0.10 Across Pressurizer Vessel Nodes Differential Press. (psi) Time (sec) 52 - 53 -0.04 0.038 52 - 54 -0.23 0.046 53 - 54 -0.20 0.050 Containment Functional Design 6.2.1-117
WATTS BAR WBNP-112 Table 6.2.1-30 Mass And Energy Release Rates 127 in2 Cold Leg (Page 1 of 5)
Time Mass Flow Energy Flow Avg. Enthalpy (sec) (lbm/sec) (Btu/sec) (Btu/lbm) 0.00000 0. 0. 0.00 0.00251 1.1982845E+04 6.7296740E+06 561.61 0.00502 1.5308269E+04 8.5974676E+06 561.62 0.00751 1.7398501E+04 9.7720743E+06 561.66 0.01001 1.9131092E+04 1.0741761E+07 561.48 0.01253 1.9948352E+04 1.1193906E+07 561.14 0.01503 1.9716482E+04 1.1050978E+07 560.49 0.01753 2.1905036E+04 1.2288321E+07 560.98 0.02006 2.2170478E+04 1.2426731E+07 560.51 0.02255 2.1560830E+04 1.2069870E+07 559.81 0.02506 2.1315153E+04 1.1923450E+07 559.39 0.02751 2.1626356E+04 1.2094688E+07 559.26 0.03001 2.1729350E+04 1.2147779E+07 559.05 0.03254 2.2084361E+04 1.2345775E+07 559.03 0.03503 2.2542872E+04 1.2603165E+07 559.08 0.03757 2.2895385E+04 1.2800602E+07 559.09 0.04009 2.3203939E+04 1.2973383E+07 559.10 0.04255 2.3446963E+04 1.3108981E+07 559.09 0.04502 2.3464854E+04 1.3115753E+07 558.95 0.04752 2.3298089E+04 1.3017402E+07 558.73 0.05001 2.3145127E+04 1.2927663E+07 558.55 0.05266 2.3018004E+04 1.2853122E+07 558.39 0.05514 2.2950194E+04 1.2812973E+07 558.29 0.05757 2.2904460E+04 1.2785675E+07 558.22 0.06012 2.2779154E+04 1.2713027E+07 558.10 0.06257 2.2510846E+04 1.2559119E+07 557.91 0.06500 2.2164087E+04 1.2360966E+07 557.70 0.06763 2.1888594E+04 1.2203861E+07 557.54 0.07009 2.1850009E+04 1.2182079E+07 557.53 0.07259 2.2019590E+04 1.2278820E+07 557.63 0.07503 2.2242956E+04 1.2406073E+07 557.75 0.07759 2.2352310E+04 1.2468054E+07 557.80 0.08002 2.2278656E+04 1.2425609E+07 557.74 0.08253 2.2036897E+04 1.2287536E+07 557.59 0.08504 2.1670113E+04 1.2078517E+07 557.38 0.08752 2.1266578E+04 1.1848983E+07 557.16 0.09004 2.0857542E+04 1.1617001E+07 556.97 0.09260 2.0466616E+04 1.1395523E+07 556.79 0.09500 2.0201194E+04 1.1245397E+07 556.67 0.09751 2.0053059E+04 1.1161858E+07 556.62 0.10007 2.0025022E+04 1.1146521E+07 556.63 6.2.1-118 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-30 Mass And Energy Release Rates 127 in2 Cold Leg (Page 2 of 5)
Time Mass Flow Energy Flow Avg. Enthalpy (sec) (lbm/sec) (Btu/sec) (Btu/lbm) 0.10515 2.0170943E+04 1.1230305E+07 556.76 0.11011 2.0365487E+04 1.1341279E+07 556.89 0.11505 2.0647554E+04 1.1501747E+07 557.05 0.12008 2.0944972E+04 1.1670752E+07 557.21 0.12502 2.0977664E+04 1.1688856E+07 557.20 0.13007 2.0780412E+04 1.1576250E+07 557.08 0.13509 2.0500682E+04 1.1417226E+07 557.92 0.14001 2.0096382E+04 1.1187990E+07 556.72 0.14508 1.9569603E+04 1.0889944E+07 556.47 0.15009 1.9235427E+04 1.0701397E+07 556.34 0.15504 1.9138491E+04 1.0647134E+07 556.32 0.16006 1.9034644E+04 1.0588880E+07 556.30 0.16505 1.8879080E+04 1.0501358E+07 556.24 0.17007 1.8748148E+04 1.0427857E+07 556.21 0.17514 1.8720580E+04 1.0412805E+07 556.22 0.18005 1.8785810E+04 1.0450146E+07 556.28 0.18504 1.8911550E+04 1.0521664E+07 556.36 0.19010 1.9101126E+04 1.0629209E+07 556.47 0.19507 1.9311878E+04 1.0748514E+07 556.58 0.20009 1.9465602E+04 1.0835436E+07 556.65 0.21252 1.9617023E+04 1.0920644E+07 556.69 0.22507 1.9458748E+04 1.0830336E+07 556.58 0.23759 1.9647389E+04 1.0937376E+07 556.68 0.25011 1.9804565E+04 1.1026138E+07 556.75 0.26253 1.9395307E+04 1.0793667E+07 556.51 0.27516 1.8760813E+04 1.0435112E+07 556.22 0.28761 1.8860759E+04 1.0492777E+07 556.33 0.30014 1.9381793E+04 1.0787950E+07 556.60 0.31261 1.9557340E+04 1.0886714E+07 556.66 0.32509 1.9428795E+04 1.0813221E+07 556.56 0.33757 1.9460687E+04 1.0831309E+07 556.57 0.35003 1.9510288E+04 1.0859152E+07 556.59 0.36251 1.9334731E+04 1.0759415E+07 556.48 0.37512 1.9237392E+04 1.0704384E+07 556.44 0.38764 1.9172556E+04 1.0667882E+07 556.41 0.40007 1.9255351E+04 1.0715044E+07 556.47 0.41263 1.9518505E+04 1.0864131E+07 556.61 0.42512 1.9566788E+04 1.0890843E+07 556.60 0.43769 1.9443279E+04 1.0820460E+07 556.51 0.45005 1.9309158E+04 1.0744438E+07 556.44 0.46260 1.9325193E+04 1.0753755E+07 556.46 Containment Functional Design 6.2.1-119
WATTS BAR WBNP-112 Table 6.2.1-30 Mass And Energy Release Rates 127 in2 Cold Leg (Page 3 of 5)
Time Mass Flow Energy Flow Avg. Enthalpy (sec) (lbm/sec) (Btu/sec) (Btu/lbm) 0.47515 1.9427001E+04 1.0811564E+07 556.52 0.48751 1.9463982E+04 1.0832327E+07 556.53 0.50010 1.9412566E+04 1.0802979E+07 556.49 0.52505 1.9416927E+04 1.0805655E+07 556.51 0.55001 1.9520981E+04 1.0864335E+07 556.55 0.57500 1.9439249E+04 1.0817886E+07 556.50 0.60009 1.9432289E+04 1.0814194E+07 556.51 0.62502 1.9570908E+04 1.0892620E+07 556.57 0.65001 1.9484134E+04 1.0843384E+07 556.52 0.67502 1.9537413E+04 1.0873742E+07 556.56 0.70006 1.9557525E+04 1.0885106E+07 556.57 0.72503 1.9556471E+04 1.0884559E+07 556.57 0.75008 1.9566953E+04 1.0890551E+07 556.58 0.77503 1.9575425E+04 1.0895394E+07 556.59 0.80011 1.9613175E+04 1.0916838E+07 556.61 0.82503 1.9623035E+04 1.0922366E+07 556.61 0.85012 1.9607042E+04 1.0913377E+07 556.60 0.87505 1.9625149E+04 1.0923689E+07 556.62 0.90005 1.9642366E+04 1.0933451E+07 556.63 0.92504 1.9652418E+04 1.0939158E+07 556.63 0.95005 1.9665495E+04 1.0946566E+07 556.64 0.97509 1.9657157E+04 1.0941870E+07 556.64 1.00024 1.9674801E+04 1.0951903E+07 556.65 1.02501 1.9674211E+04 1.0951587E+07 556.65 1.05002 1.9685832E+04 1.0958208E+07 556.65 1.07501 1.9689581E+04 1.0960360E+07 556.66 1.10003 1.9688612E+04 1.0959861E+07 556.66 1.12501 1.9688440E+04 1.0959833E+07 556.66 1.15013 1.9691682E+04 1.0961746E+07 556.67 1.17512 1.9694412E+04 1.0963374E+07 556.67 1.20008 1.9690643E+04 1.0961334E+07 556.68 1.22506 1.9686074E+04 1.0958870E+07 556.68 1.25010 1.9682378E+04 1.0956913E+07 556.69 1.27506 1.9685597E+04 1.0958900E+07 556.70 1.30002 1.9688096E+04 1.0960455E+07 556.70 1.32505 1.9673388E+04 1.0952302E+07 556.71 1.35006 1.9668391E+04 1.0949690E+07 556.72 1.37504 1.9669445E+04 1.0950509E+07 556.73 1.40009 1.9673705E+04 1.0950139E+07 556.74 1.42508 1.9668652E+04 1.0950505E+07 556.75 1.45004 1.9667081E+04 1.0950053E+07 556.76 6.2.1-120 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-30 Mass And Energy Release Rates 127 in2 Cold Leg (Page 4 of 5)
Time Mass Flow Energy Flow Avg. Enthalpy (sec) (lbm/sec) (Btu/sec) (Btu/lbm) 1.47501 1.9675943E+04 1.0955165E+07 556.78 1.50004 1.9668050E+04 1.0950970E+07 556.79 1.52500 1.9665596E+04 1.0949895E+07 556.80 1.55005 1.9671043E+04 1.0953307E+07 556.82 1.57502 1.9666568E+04 1.0951104E+07 556.84 1.60008 1.9662702E+04 1.0949279E+07 556.86 1.62509 1.9658419E+04 1.0947234E+07 556.87 1.65008 1.9652327E+04 1.0944186E+07 556.89 1.67508 1.9641445E+04 1.0938449E+07 556.91 1.70000 1.9631684E+04 1.0933366E+07 556.92 1.72523 1.9622211E+04 1.0928465E+07 556.94 1.75002 1.9611372E+04 1.0922805E+07 556.96 1.77506 1.9600265E+04 1.0917009E+07 556.98 1.80004 1.9586316E+04 1.0909616E+07 556.00 1.82507 1.9570844E+04 1.0901377E+07 557.02 1.85004 1.9558044E+04 1.0894662E+07 557.04 1.87501 1.9547428E+04 1.0889183E+07 557.06 1.90005 1.9533703E+04 1.0881955E+07 557.09 1.92505 1.9518588E+04 1.0873945E+07 557.11 1.95013 1.9504270E+04 1.0866400E+07 557.13 1.97508 1.9490671E+04 1.0854264E+07 557.15 2.00001 1.9475975E+04 1.0851512E+07 557.17 2.02504 1.9460138E+04 1.0843124E+07 557.20 2.05011 1.9443525E+04 1.0834315E+07 557.22 2.07503 1.9425610E+04 1.0824775E+07 557.24 2.10004 1.9406458E+04 1.0814547E+07 557.27 2.12507 1.9386749E+04 1.0804030E+07 557.29 2.15003 1.9366596E+04 1.0793269E+07 557.31 2.17504 1.9344857E+04 1.0781622E+07 557.34 2.20000 1.9321966E+04 1.0769339E+07 557.36 2.22510 1.9298174E+04 1.0756568E+07 557.39 2.25001 1.9274722E+04 1.0743996E+07 557.41 2.27507 1.9250836E+04 1.0731182E+07 557.44 2.30008 1.9225729E+04 1.0717684E+07 557.47 2.32510 1.9199767E+04 1.0703706E+07 557.49 2.35000 1.9189974E+04 1.0698897E+07 557.53 2.37503 1.9159580E+04 1.0682347E+07 557.55 2.40011 1.9117138E+04 1.0659079E+07 557.57 2.42510 1.9108543E+04 1.0654963E+07 557.60 2.45013 1.9096201E+04 1.0648650E+07 557.63 2.47510 1.9042948E+04 1.0633130E+07 557.65 Containment Functional Design 6.2.1-121
WATTS BAR WBNP-112 Table 6.2.1-30 Mass And Energy Release Rates 127 in2 Cold Leg (Page 5 of 5)
Time Mass Flow Energy Flow Avg. Enthalpy (sec) (lbm/sec) (Btu/sec) (Btu/lbm) 2.50011 1.9042948E+04 1.0619918E+07 557.68 2.52510 1.9038224E+04 1.0617984E+07 557.72 2.55010 1.9011234E+04 1.0603416E+07 557.74 2.57508 1.8977430E+04 1.0585017E+07 557.77 2.60006 1.8963744E+04 1.0578049E+07 557.80 2.62512 1.8950653E+04 1.0571411E+07 557.84 2.65025 1.8927642E+04 1.0559161E+07 557.87 2.67504 1.8894421E+04 1.0541167E+07 557.90 2.70018 1.8869044E+04 1.0527674E+07 557.93 2.72514 1.8846108E+04 1.0515517E+07 557.97 2.75003 1.8827068E+04 1.0505586E+07 558.00 2.77504 1.8815133E+04 1.0499666E+07 558.04 2.80005 1.8795707E+04 1.0489482E+07 558.08 2.82511 1.8768598E+04 1.0474967E+07 558.11 2.85006 1.8741259E+04 1.0460340E+07 558.14 2.87505 1.8723005E+04 1.0450857E+07 558.18 2.90005 1.8704799E+04 1.0441382E+07 558.22 2.92505 1.8678392E+04 1.0427269E+07 558.25 2.95003 1.8650919E+04 1.0412569E+07 558.29 2.97508 1.8627102E+04 1.0399953E+07 558.32 3.00020 1.8605296E+04 1.0388476E+07 558.36 6.2.1-122 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-31 Reactor Cavity Volumes (Page 1 of 2)
COMPARTMENT NUMBER COMPARTMENT LOCATION VOLUME (ft3) 1 Break Location 164.595 2 Lower Reactor Cavity 12,000.
3 Reactor Vessel Annulus 1.319 4 Reactor Vessel Annulus 1.938 5 Reactor Vessel Annulus 8.601 6 Reactor Vessel Annulus 8.601 7 Reactor Vessel Annulus 9.825 8 Reactor Vessel Annulus 17.202 9 Reactor Vessel Annulus 9.825 10 Reactor Vessel Annulus 17.202 11 Reactor Vessel Annulus 9.205 12 Reactor Vessel Annulus 17.202 13 Reactor Vessel Annulus 9.206 14 Reactor Vessel Annulus 17.202 15 Reactor Vessel Annulus 9.825 16 Reactor Vessel Annulus 17.202 17 Reactor Vessel Annulus 9.825 18 Reactor Vessel Annulus 17.202 19 Reactor Vessel Annulus 9.206 20 Reactor Vessel Annulus 17.202 21 Lower Containment 60,000.
22 Lower Containment 60,000.
23 Lower Containment 60,000.
24 Lower Containment 60,000.
25 Break Location 165.206 26 Inspection Annulus 165.819 27 Inspection Annulus 165.206 28 Inspection Annulus 164.595 29 Inspection Annulus 165.206 30 Inspection Annulus 165.819 31 Inspection Annulus 165.206 32 Upper Containment 651,000.
33 Reactor Vessel Annulus 1.404 34 Reactor Vessel Annulus 1.404 35 Reactor Vessel Annulus 1.938 36 Reactor Vessel Annulus 8.601 37 Reactor Vessel Annulus 8.601 38 Reactor Vessel Annulus 17.202 39 Reactor Vessel Annulus 17.202 40 Reactor Vessel Annulus 17.202 41 Reactor Vessel Annulus 17.202 42 Reactor Vessel Annulus 17.202 43 Reactor Vessel Annulus 17.202 44 Reactor Vessel Annulus 17.202 45 Reactor Vessel Annulus 0.602 46 Reactor Vessel Annulus 0.602 47 Upper Reactor Cavity 15,500.
48 Ice Condenser 24,241.
Containment Functional Design 6.2.1-123
WATTS BAR WBNP-112 Table 6.2.1-31 Reactor Cavity Volumes (Page 2 of 2)
COMPARTMENT NUMBER COMPARTMENT LOCATION VOLUME (ft3) 49 Ice Condenser 28,760.
50 Ice Condenser 28,760.
51 Ice Condenser 28,760.
52 Ice Condenser 47,000.
53 Pipe Annulus 150.
54 Inspection Port 17.280 55 Inspection Port 17.280 56 Inspection Port 17.280 57 Inspection Port 17.280 58 Inspection Port 17.280 59 Inspection Port 17.280 60 Inspection Port 17.280 61 Inspection Port 17.280 62 Pipe Annulus 47.
63 Pipe Annulus 47.
64 Pipe Annulus 47.
65 Pipe Annulus 47.
66 Pipe Annulus 47.
67 Pipe Annulus 47.
68 Pipe Annulus 150.
6.2.1-124 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-32 Flow Path Data (Reactor Cavity) (Page 1 of 3)
Inertia Hydraulic Flow Equiv. Area Length Diameter Area Length Ratio Between Compartments k f (ft) (ft) (ft2) (ft) a/A 1 to 3 0.4 0.02 1.6 0.3 2.7 1.2 0.28 2 to 22 2.9 0.02 28. 5.8 36. 19. 0.0 3 to 34 1.0 0.02 0.7 0.4 1.2 0.7 1.0 4 to 35 0.0 0.02 3.6 0.4 0.7 3.6 1.0 5 to 36 0.0 0.02 3.3 0.4 2.6 3.3 1.0 6 to 37 0.0 0.02 3.3 0.4 2.6 3.3 1.0 7 to 9 1.0 0.02 4.9 0.4 1.0 4.1 1.0 8 to 10 0.0 0.02 6.6 0.4 2.6 6.6 1.0 9 to 11 1.04 0.02 4.6 0.4 1.0 3.7 0.46 10 to 12 0.0 0.02 6.6 0.4 2.6 6.6 1.0 11 to 13 1.04 0.02 4.8 0.4 1.0 4.0 0.46 12 to 14 0.0 0.02 6.6 0.4 2.6 6.6 1.0 13 to 15 1.04 0.02 4.6 0.4 1.0 3.7 0.46 14 to 16 0.0 0.02 6.6 0.4 2.6 6.6 1.0 15 to 17 1.04 0.02 4.9 0.4 1.0 4.1 0.5 16 to 18 0.0 0.02 6.6 0.4 2.6 6.6 1.0 17 to 19 1.0 0.02 4.6 0.4 1.0 3.7 0.46 18 to 20 0.0 0.02 6.6 0.4 2.6 6.6 1.0 19 to 4 1.0 0.02 5.4 0.4 0.5 5.4 1.0 20 to 6 0.0 0.02 5.0 0.4 2.6 5.0 1.0 21 to 22 2.0 0.02 38. 40. 1560. 38. 0.43 22 to 23 3.0 0.02 38. 40. 1560. 38. 0.47 23 to 24 2.0 0.02 38. 40. 1560. 38. 0.43 24 to 21 3.0 0.02 32. 8.0 100. 27. 0.09 25 to 7 2.8 0.02 3.0 0.2 1.1 1.7 0.12 26 to 9 2.8 0.02 3.0 0.2 1.1 1.7 0.12 27 to 11 2.8 0.02 3.1 0.2 1.3 1.7 0.13 28 to 13 2.8 0.02 3.1 0.2 1.3 1.7 0.13 29 to 15 2.8 0.02 3.0 0.2 1.1 1.7 0.12 30 to 17 2.8 0.02 3.0 0.2 1.1 1.7 0.12 31 to 19 2.8 0.02 3.1 0.2 1.3 1.7 0.13 33 to 3 1.0 0.02 0.7 0.4 1.2 0.7 0.99 34 to 7 1.0 0.02 3.6 0.4 1.2 3.3 0.66 35 to 7 1.0 0.02 5.4 0.4 0.5 5.4 1.0 36 to 38 0.0 0.02 5.0 0.4 2.2 5.0 1.0 37 to 8 0.0 0.02 5.0 0.4 2.6 5.0 1.0 38 to 39 0.0 0.02 6.6 0.4 2.6 6.6 1.0 39 to 40 0.0 0.02 6.6 0.4 2.6 6.6 1.0 40 to 41 0.0 0.02 6.6 0.4 2.6 6.6 1.0 41 to 42 0.0 0.02 6.6 0.4 2.6 6.6 1.0 42 to 43 0.0 0.02 6.6 0.4 2.6 6.6 1.0 43 to 44 0.0 0.02 6.6 0.4 2.6 6.6 1.0 44 to 5 0.0 0.02 5.0 0.4 2.6 5.0 1.0 45 to 3 1.0 0.02 0.8 0.4 0.5 0.8 0.78 46 to 3 1.0 0.02 0.8 0.4 0.5 0.8 0.78 53 to 1 0.4 0.02 7.6 0.83 5.5 6.8 0.11 54 to 1 0.5 0.02 2.6 2.5 4.9 1.9 0.25 55 to 25 0.5 0.02 2.6 2.5 4.9 1.9 0.25 56 to 26 0.5 0.02 2.6 2.5 4.9 2.0 0.26 Containment Functional Design 6.2.1-125
WATTS BAR WBNP-112 Table 6.2.1-32 Flow Path Data (Reactor Cavity) (Page 2 of 3)
Inertia Hydraulic Flow Equiv. Area Length Diameter Area Length Ratio Between Compartments k f (ft) (ft) (ft2) (ft) a/A 57 to 27 0.5 0.02 2.6 2.5 4.9 1.9 0.25 58 to 28 0.5 0.02 2.6 2.5 4.9 1.9 0.25 59 to 29 0.5 0.02 2.6 2.5 4.9 1.9 0.25 60 to 30 0.5 0.02 2.6 2.5 4.9 2.0 0.26 61 to 31 0.5 0.02 2.6 2.5 4.9 1.9 0.25 62 to 25 0.4 0.02 3.0 0.83 5.5 2.2 0.11 63 to 26 0.4 0.02 3.0 0.83 5.5 2.2 0.11 64 to 27 0.4 0.02 3.0 0.83 5.5 2.2 0.11 65 to 28 0.4 0.02 3.0 0.83 5.5 2.2 0.11 66 to 29 0.4 0.02 3.0 0.83 5.5 2.2 0.11 67 to 30 0.4 0.02 3.0 0.83 5.5 2.2 0.11 68 to 31 0.4 0.02 7.6 0.83 5.5 6.8 0.11 1 to 19 0.4 0.02 3.1 0.2 1.3 1.7 0.13 2 to 6 3.7 0.02 6.5 0.4 0.7 6.4 0.0 4 to 45 0.6 0.02 2.4 0.4 0.7 2.4 0.95 6 to 5 0.0 0.02 13. 0.4 0.7 13. 1.0 7 to 38 1.0 0.02 6.0 0.4 0.3 4.7 0.23 8 to 2 3.7 0.02 6.6 0.4 1.3 6.4 0.0 9 to 39 9.2 0.02 6.7 0.4 0.3 4.9 0.23 10 to 2 3.7 0.02 6.6 0.4 1.3 6.4 0.0 11 to 40 1.0 0.02 5.5 0.4 0.2 4.5 0.17 12 to 2 3.7 0.02 6.6 0.4 1.3 6.4 0.0 13 to 41 9.2 0.02 6.0 0.4 0.2 4.6 0.17 14 to 2 3.7 0.02 6.6 0.4 1.3 6.4 0.0 15 to 42 1.0 0.02 6.0 0.4 0.3 4.7 0.23 16 to 2 3.7 0.02 6.6 0.4 1.3 6.4 0.0 17 to 43 9.2 0.02 6.7 0.4 0.3 4.9 0.23 18 to 2 3.7 0.02 6.6 0.4 1.3 6.4 0.0 19 to 44 1.0 0.02 5.5 0.4 0.2 4.5 0.17 20 to 2 3.7 0.02 6.6 0.4 1.3 6.4 0.0 21 to 48 .7837 0.0 10.36 1.0 265.875 0.0 0.096 22 to 48 .7837 0.0 10.36 1.0 265.875 0.0 0.096 23 to 48 .7837 0.0 10.36 1.0 265.875 0.0 0.096 24 to 48 .7837 0.0 10.36 1.0 265.875 0.0 0.096 25 to 3 0.4 0.02 1.6 0.3 2.7 1.2 0.28 26 to 7 0.4 0.02 3.0 0.2 1.1 1.7 0.12 27 to 9 0.4 0.02 3.0 0.2 1.1 1.7 0.12 28 to 11 0.4 0.02 3.1 0.2 1.3 1.7 0.13 29 to 13 0.4 0.02 3.1 0.2 1.3 1.7 0.13 30 to 15 0.4 0.02 3.0 0.2 1.1 1.7 0.12 31 to 17 0.4 0.02 3.0 0.2 1.1 1.7 0.12 33 to 46 2.2 0.02 3.3 0.4 0.4 3.3 0.25 34 to 46 2.2 0.02 3.3 0.4 0.4 3.3 0.25 35 to 47 1.1 0.02 3.0 0.4 0.7 1.5 0.0 37 to 36 0.0 0.02 13. 0.4 0.7 13. 1.0 38 to 8 0.0 0.02 13. 0.4 1.3 13. 1.0 39 to 10 0.0 0.02 13. 0.4 1.3 13. 1.0 6.2.1-126 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-32 Flow Path Data (Reactor Cavity) (Page 3 of 3)
Inertia Hydraulic Flow Equiv. Area Length Diameter Area Length Ratio Between Compartments k f (ft) (ft) (ft2) (ft) a/A 40 to 12 0.0 0.02 13. 0.4 1.3 13. 1.0 41 to 14 0.0 0.02 13. 0.4 1.3 13. 1.0 42 to 16 0.0 0.02 13. 0.4 1.3 13. 1.0 43 to 18 0.0 0.02 13. 0.4 1.3 13. 1.0 44 to 20 0.0 0.02 13. 0.4 1.3 13. 1.0 45 to 33 0.0 0.02 3.3 0.4 0.4 3.3 0.25 48 to 49 0.0 0.1055 8.733 0.855 989.01 8.0 0.230 49 to 50 0.0 0.0592 12.278 0.855 982.47 16.0 0.239 50 to 51 0.0 0.0592 12.278 0.855 982.47 16.0 0.359 51 to 52 0.87979 0.1249 8.8558 0.855 982.47 8.0 0.359 52 to 32 1.43 0.0 2.8 1.0 2003.1 0.269 53 to 25 0.4 0.02 7.6 0.83 5.5 6.8 0.11 54 to 47 1.0 0.02 1.9 2.5 4.9 1.8 0.0 55 to 47 1.0 0.02 1.9 2.5 4.9 1.8 0.0 56 to 47 1.0 0.02 1.9 2.5 4.9 1.8 0.0 57 to 47 1.0 0.02 1.9 2.5 4.9 1.8 0.0 58 to 47 1.0 0.02 1.9 2.5 4.9 1.8 0.0 59 to 47 1.0 0.02 1.9 2.5 4.9 1.8 0.0 60 to 47 1.0 0.02 1.9 2.5 4.9 1.8 0.0 61 to 47 1.0 0.02 1.9 2.5 4.9 1.8 0.0 62 to 26 0.4 0.02 3.0 0.83 5.5 2.2 0.11 63 to 27 0.4 0.02 3.0 0.83 5.5 2.2 0.11 64 to 28 0.4 0.02 3.0 0.83 5.5 2.2 0.11 65 to 29 0.4 0.02 3.0 0.83 5.5 2.2 0.11 66 to 30 0.4 0.02 3.0 0.83 5.5 2.2 0.11 67 to 31 0.4 0.02 3.0 0.83 5.5 2.2 0.11 68 to 1 0.4 0.02 7.6 0.83 5.5 8.8 0.11 1 to 25 1.0 0.02 5.4 1.5 9.6 2.6 0.47 2 to 37 3.7 0.02 6.5 0.4 0.7 6.4 0.0 4 to 47 1.1 0.02 3.0 0.4 0.7 1.5 1.0 5 to 46 9.2 0.02 7.8 2.0 0.5 18. 1.0 7 to 47 1.1 0.02 3.0 0.4 1.4 2.9 0.0 9 to 47 1.1 0.02 3.0 0.4 1.4 2.9 0.0 11 to 47 1.1 0.02 3.0 0.4 1.4 2.9 0.0 13 to 47 1.1 0.02 3.0 0.4 1.4 2.9 0.0 15 to 47 1.1 0.02 3.0 0.4 1.4 2.9 0.0 17 to 47 1.1 0.02 3.0 0.4 1.4 2.9 0.0 19 to 47 1.1 0.02 3.0 0.4 1.4 2.9 0.0 21 to 47 3.8 0.02 5.8 5.1 26. 4.0 0.04 22 to 47 3.8 0.02 9.1 12. 74. 4.2 0.10 23 to 47 3.8 0.02 8.3 11. 62. 4.0 0.08 24 to 47 3.9 0.02 6.3 5.5 32. 4.0 0.04 25 to 26 1.0 0.02 5.3 1.4 9.1 2.3 0.44 26 to 27 1.0 0.02 5.3 1.4 9.1 2.6 0.44 27 to 28 1.0 0.02 5.4 1.5 9.6 2.6 0.47 28 to 29 1.0 0.02 5.4 1.5 9.6 2.6 0.47 29 to 30 1.0 0.02 5.3 1.4 9.1 2.6 0.44 30 to 31 1.0 0.02 5.3 1.4 9.1 2.6 0.44 31 to 1 1.0 0.02 5.4 1.5 9.6 2.6 0.47 33 to 19 1.0 0.02 3.6 0.4 1.2 3.3 0.61 35 to 46 0.6 0.02 2.4 0.4 0.7 2.4 0.95 36 to 46 9.2 0.02 7.8 2.0 0.5 18. 0.95 45 to 34 0.0 0.02 3.3 0.4 0.4 3.3 0.25 53 to 21 1.0 0.02 7.2 17. 11.0 8.8 0.0 62 to 21 1.0 0.02 2.5 1.5 11.0 2.1 0.0 63 to 22 1.0 0.02 2.5 1.5 11.0 2.1 0.0 64 to 22 1.0 0.02 2.5 1.7 11.0 2.1 0.0 65 to 23 1.0 0.02 2.5 1.7 11.0 2.1 0.0 66 to 23 1.0 0.02 2.5 1.5 11.0 2.1 0.0 67 to 24 1.0 0.02 2.5 1.5 11.0 2.1 0.0 68 to 24 1.0 0.02 7.2 1.7 11.0 6.8 0.0 Containment Functional Design 6.2.1-127
WATTS BAR WBNP-112 Table 6.2.1-33 Containment Data (ECCS Analysis)
(Page 1 of 2)
I. Conservatively High Estimate of Containment Net Free Volume Containment Area Volume (ft3)
Upper Compartment 651,000 Lower Compartment 271,400 Ice Condenser 169,400 Dead-Ended Compartments (includes all accumulator rooms, both 129,900 fan compartments, instrument room pipe tunnel)
II. Initial Conditions A. Containment Pressure 15.0 psia B. Lowest Operational Containment Temperature for the Upper, 85°F Lower, and Dead-Ended Compartments 100°F C. Highest Refueling Water Storage Tank Temperature 100°F D. Lowest Temperature Outside Containment 5°F E. Highest Initial Spray Temperature 100°F F. Lowest Annulus Temperature 40°F III. Structural Heat Sinks**
A. For Each Surface
- 1. Description of Surface
- 2. Conservatively High Estimate of Area Exposed to Containment See Tables 6.2.1-34 Atmosphere through 6.2.1-36
- 3. Location in Containment by Compartment B. For Each Separate Layer of Each Surface
- 1. Material
- 2. Conservatively Large Estimate of Layer Thickness See Tables 6.2.1-34 through 6.2.1-36
- 3. Conservatively High Value of Material Conductivity See Tables 6.2.1-34 through 6.2.1-36
- 4. Conservatively High Value of Volumetric Heat Capacity See Tables 6.2.1-34 through 6.2.1-36 6.2.1-128 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-33 Containment Data (ECCS Analysis)
(Page 2 of 2)
IV. Spray System A. Runout Flow for a Spray Pump*** (Containment Spray) 7700 gpm B. Number of Spray Pumps Operating with No Diesel Failure 2/Unit C. Number of Spray Pumps Operating with One Diesel Failure 1/Unit D. Assumed Post Accident Initiation of Spray System 25 sec V. Deck Fan A. Fastest Post Accident Initiation of Deck Fans 10 min B. Conservatively High Flow Rate Per Fan 42,000 cfm VI. Conservatively Low Hydrogen Skimmer System Flow Rate 100 cfm/each
- Structural heat sinks should also account for any surfaces neglected in containment integrity analysis.
- Runout flow is for a break immediately downstream of the pump. In that event, the spray water will not enter the containment.
Containment Functional Design 6.2.1-129
WATTS BAR WBNP-112 Table 6.2.1-34 Major Characteristics Of Structural Heat Sinks Inside Sequoyah Nuclear Plant Containment - Upper Compartment Heat Thickness Volume Transfer and Thermal Heat Area Material Conductivity Capacity Structure (ft2) (as noted) (Btu/ft-hr-°F) (Btu/ft3-°F)
Operating Deck 4,452 1.1 ft concrete 0.84 30.24 7,749 6.3 mils coating 0.087 29.8 1.1 ft concrete 0.84 30.24 672 1.6 ft concrete 0.84 30.24 11,445 6.3 mils coating 0.087 29.8 1.6 ft concrete 0.84 30.24 4,032 0.26 in. stainless steel 9.87 59.22 1.6 ft concrete 0.84 30.24 798 15.7 mils coating 0.087 29.8 1.6 ft concrete 0.84 30.24 Containment Shell 22,890 7.8 mils coating 0.21 29.8 0.46 in. carbon steel 27.3 30.24 18,375 7.8 mils coating 0.21 29.8 0.58 in. carbon steel 27.3 59.22 2,100 7.8 mils coating 0.21 29.8 1.51 in. carbon steel 27.3 59.22 Miscellaneous Steel 4,095 7.8 mils coating 0.21 29.8 0.26 in. carbon steel 27.3 59.22 3,559 7.8 mils coating 0.21 29.8 0.46 in. carbon steel 27.3 59.22 3,539 7.8 mils coating 0.21 29.8 0.72 in. carbon steel 27.3 59.22 273 7.8 mils coating 0.21 29.8 1.57 in. carbon steel 27.3 59.2 6.2.1-130 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-35 Major Characteristics Of Structural Heat Sinks Inside Sequoyah Nuclear Plant Containment - Lower Compartment (Page 1 of 2)
Heat Thickness Volume Transfer and Thermal Heat Area Material Conductivity Capacity Structure (ft2) (as noted) (Btu/ft-hr-°F) (Btu/ft3-°F)
Operating Deck 7,507 1.1 ft concrete 0.84 30.24 2,971 1.6 mils coating 0.087 29.8 1.1 ft concrete 0.84 30.24 2,131 1.6 ft concrete 0.84 30.24 789 6.3 mils coating 0.087 29.8 1.84 ft concrete 0.84 30.24 2,646 2.1 ft concrete 0.84 30.24 210 6.3 mils coating 0.087 29.8 2.1 ft concrete 0.84 30.24 Crane Wall 14,752 1.6 ft concrete 0.84 30.24 3,570 6.3 mils coating 0.087 29.8 1.6 ft concrete 0.84 30.24 Containment Floor 567 1.6 ft concrete 0.84 30.24 7,612 6.3 mils coating 0.087 29.8 1.6 ft concrete 0.84 30.24 Interior Concrete 3,780 1.1 ft concrete 0.84 30.24 567 1.1 ft concrete 0.84 30.24 2,992 2.1 ft concrete 0.84 30.24 2,384 0.26 in. stainless 9.8 59.2 steel 2.1 ft concrete 0.84 30.24 2,373 2.1 ft concrete 0.84 30.24 1,480 6.3 mils coating 0.087 29.8 2.1 ft concrete 0.84 30.24 Miscellaneous Steel 12,915 7.8 mils coating 0.22 14.7 0.53 in. carbon steel 27.3 59.2 7,560 7.8 mils coating 0.22 14.7 0.78 in. carbon steel 27.3 59.2 5,250 7.8 mils coating 0.22 14.7 1.1 carbon steel 27.3 59.2 Containment Functional Design 6.2.1-131
WATTS BAR WBNP-112 Table 6.2.1-35 Major Characteristics Of Structural Heat Sinks Inside Sequoyah Nuclear Plant Containment - Lower Compartment (Page 2 of 2)
Heat Thickness Volume Transfer and Thermal Heat Area Material Conductivity Capacity Structure (ft2) (as noted) (Btu/ft-hr-°F) (Btu/ft3-°F) 2,625 7.8 mils coating 0.22 14.7 1.45 in. carbon steel 27.3 59.2 1,575 7.8 mils coating 0.22 14.7 1.7 in. carbon steel 27.3 59.2 6.2.1-132 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-36 Major Characteristics Of Structural Heat Sinks Inside Sequoyah Nuclear Plant Containment - Dead-Ended Compartment Heat Thickness and Thermal Volume Heat Transfer Material (as noted) Conductivity (Btu/ft- Capacity Structure Area (ft2) hr-°F) (Btu/ft3-°F)
Containment Shell 3,045 7.8 mils coating 0.22 14.7 0.78 in. carbon steel 27.3 59.2 4,305 7.8 mils coating 0.22 14.7 1.1 in. carbon steel 27.3 59.2 4,305 7.8 mils coating 0.22 14.7 1.25 in. carbon steel 27.3 59.2 3,780 7.8 mils coating 0.22 14.7 1.37 in. carbon steel 27.3 59.2 4,305 7.8 mils coating 0.22 14.7 1.51 in. carbon steel 27.3 59.2 Crane Wall 7,255 1.6 ft concrete 0.84 30.24 3,801 6.3 mils coating 0.87 14.7 1.58 ft concrete 0.84 30.24 Containment Floor 4,809 6.3 mils coating 0.087 14.7 2.1 ft concrete 0.84 30.24 Interior Concrete 9,870 1.1 ft concrete 0.84 30.24 3,948 6.3 mils coating 0.087 14.7 1.1 ft concrete 0.84 30.24 5,376 1.58 ft concrete 0.84 30.24 Containment Functional Design 6.2.1-133
WATTS BAR WBNP-112 Table 6.2.1-37 Maximum Reverse Pressure Differential Pressure Analysis Base Case Westinghouse ECCS structural heat transfer model Sprays at runout flow Offsite power available spray start time Minimum containment temperature Dead-ended volume is swept Max. reverse differential pressure = 0.65 psi Case Variable Change in Max. dP (psi) 1 Ice condenser flow through the drains acts as 50% thermal +0.2 efficient spray 2 Same as Case 1, except 100% thermal efficiency +0.4 3 Maximum containment temperature -0.2 4 Heat transfer coefficient to sump equals 5 times Hmax <0.1 5 Same as Case 2, except drain flow rate times 1.5 +0.6 6 Combination of Cases 2 and 4 +0.4 7 1 bay of ice condenser doors remains open -0.65 8 Same as Case 6 except Equation (3) written as +0.55 H = Hstag + [Hmax - Hstag] e-.025 [t-tp]
9 Same as Case 6 except 5 times upper to lower resistance +2.0 10 RWST temperature = 105°F +0.2 6.2.1-134 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-38 Ice Condenser Steam Exit Flow vs. Time vs. Sump Temperature (Page 1 of 3)
Ice Condenser Steam Exit Flow Time (sec) Sump Temp. (°F) (lb/sec) 13.1 190.3 -1.74 13.8 190.6 -1.63 14.4 190.7 -1.76 15.0 190.9 -1.54 15.4 191.1 -1.37 15.9 191.2 -1.23 16.3 191.3 -.13 16.6 191.4 -.09 17.0 191.5 -.09 17.4 191.6 -.08 17.8 191.7 -.08 18.2 191.8 -.07 18.6 191.9 -.07 19.0 192.0 -.07 19.3 192.1 -.07 19.7 192.2 -.06 20.0 192.3 -1.04 20.3 192.4 -.93 20.9 192.5 -1.17 21.5 192.7 -1.43 21.8 192.8 -2.24 22.4 192.9 -2.95 23.0 193.1 -2.85 23.6 193.2 -2.64 23.9 193.3 -2.53 24.5 193.4 -2.34 25.1 193.8 -2.17 25.4 194.0 -2.05 25.7 194.1 -1.94 26.0 194.2 -1.85 Containment Functional Design 6.2.1-135
WATTS BAR WBNP-112 Table 6.2.1-38 Ice Condenser Steam Exit Flow vs. Time vs. Sump Temperature (Page 2 of 3)
Ice Condenser Steam Exit Flow Time (sec) Sump Temp. (°F) (lb/sec) 26.6 194.6 -1.69 27.2 194.8 -1.58 27.5 194.9 -1.53 28.0 195.2 -1.45 29.5 195.6 -1.40 30.1 195.8 -1.42 30.7 196.0 -1.44 31.3 196.2 -1.45 31.9 196.3 -1.45 32.5 196.4 -1.43 33.1 196.5 -1.40 33.7 196.6 -1.36 34.3 196.8 -1.31 34.9 196.9 -1.26 35.5 196.9 -1.20 36.0 197.0 -1.115 36.9 197.2 -0.96 37.9 197.3 -0.80 38.9 197.4 -0.63 40.1 197.4 -0.44 41.3 197.5 -0.29 42.2 197.5 -0.20 44.0 197.4 -.09 44.9 197.3 -0.4 45.4 197.3 .12 46.7 197.2 .19 47.6 197.0 .20 48.9 196.9 .19 49.8 196.7 .17 51.2 196.5 .12 6.2.1-136 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-38 Ice Condenser Steam Exit Flow vs. Time vs. Sump Temperature (Page 3 of 3)
Ice Condenser Steam Exit Flow Time (sec) Sump Temp. (°F) (lb/sec) 52.3 196.4 .07 53.6 196.1 .01 54.4 196.0 -.01 55.2 195.9 -.03 56.2 195.7 -.05 57.1 195.5 -.07 58.0 195.4 -.10 59.0 195.2 -.17 59.9 195.0 -.14 60.9 194.9 -.15 61.6 194.7 -.17 62.8 194.5 -.18 63.7 194.3 -.20 64.7 194.2 -.22 65.6 194.0 -.24 66.6 193.8 -.31 67.5 193.6 -.41 68.4 193.5 -.60 69.4 193.3 .20 70.3 193.2 .63 71.3 193.0 .84 72.2 192.9 1.05 73.2 192.7 1.25 74.1 192.6 1.39 75.1 192.5 1.54 76.0 192.4 1.66 77.0 192.3 1.78 Containment Functional Design 6.2.1-137
WATTS BAR WBNP-112 t
Table 6.2.1-39 Mass and Energy Release Rates For Specified Steam Line Breaks I. Run 1 - 1.4 ft² Break, 100.6% Power, AFW Runout Protection Failure Mass Flow Rate Energy Flow Rate Time (sec) (lbm/sec) (Btu/sec) 0.01 12704.8 15143070.0 0.6 12618.8 15043683.0 1.00 12553.8 14969156.0 2.0 12405.8 14798220.0 3.0 12272.8 14642025.0 4.0 11312.0 13487580.0 5.0 10363.0 12391015.0 6.0 9590.0 11481560.0 7.0 9215.0 11041828.0 8.2 8940.0 10721244.0 8.4 8896.0 10668477.0 10.0 8594.0 10314893.0 11.0 8408.0 10091639.0 12.0 8203.0 9853781.0 12.4 8112.0 9744465.0 12.6 1940.0 2331880.0 14.0 1846.0 2218892.0 17.6 1624.0 1955296.0 20.0 1502.0 1808408.0 25.2 1310.0 1577240.0 30.2 1177.0 1417108.0 35.2 1082.0 1302728.0 45.20 970.3 1168241.0 60.2 887.7 1067903.0 90.2 812.5 976625.0 150.2 760.3 913880.6 200.2 746.5 897293.0 250.2 730.7 877570.7 300.2 615.1 737504.9 312.2 515.7 617292.9 6.2.1-138 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-39 Mass and Energy Release Rates For Specified Steam Line Breaks I. Run 1 - 1.4 ft² Break, 100.6% Power, AFW Runout Protection Failure Mass Flow Rate Energy Flow Rate Time (sec) (lbm/sec) (Btu/sec) 326.2 416.4 496765.2 368.2 315.0 374220.0 420.2 308.6 366616.8 500.2 308.1 366022.8 600.2 307.9 365785.2 604.2 329.1 391299.9 606.2 223.5 264177.0 612.2 116.9 136656.1 622.2 58.11 67175.16 700.2 0.0 0.0 Containment Functional Design 6.2.1-139
WATTS BAR WBNP-112 Table 6.2.1-39 Mass and Energy Release Rates For Specified Steam Line Breaks (Contd)
II. Run 2 - 0.6 ft² Split, 30% Power, AFW Runout Protection Failure Mass Flow Rate Energy Flow Rate Time (sec) (lbm/sec) (Btu/sec)
.1000E-01 .1375E+04 .1633E+07
.6000E+00 .1371E+04 .1628E+07
.1000E+01 .1363E+04 .1619E+07
.2000E+01 .1345E+04 .1599E+07
.3000E+01 .1330E+04 .1581E+07
.4000E+01 .1315E+04 .1564E+07
.5000E+01 .1300E+04 .1547E+07
.5400E+01 .1295E+04 .1541E+07
.6000E+01 .1300E+04 .1547E+07
.7000E+01 .1299E+04 .1546E+07
.8000E+01 .1299E+04 .1545E+07
.1220E+02 .1296E+04 .1542E+07
.1400E+02 .1292E+04 .1538E+07
.1600E+02 .1251E+04 .1491E+07
.1800E+02 .1178E+04 .1407E+07
.2000E+02 .1116E+04 .1335E+07
.2420E+02 .1018E+04 .1220E+07
.2820E+02 .9426E+03 .1131E+07
.3220E+02 .8813E+03 .1058E+07
.3620E+02 .8309E+03 .9986E+06
.4020E+02 .7886E+03 .9483E+06
.4420E+02 .7533E+03 .9063E+06
.4620E+02 .7376E+03 .8876E+06
.4820E+02 .7231E+03 .8702E+06
.5020E+02 .7095E+03 .8540E+06
.5420E+02 .6851E+03 .8248E+06
.5870E+02 .6612E+03 .7961E+06
.6620E+02 .6278E+03 .7561E+06
.7220E+02 .6056E+03 .7293E+06
.8820E+02 .5600E+03 .6745E+06 6.2.1-140 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-39 Mass and Energy Release Rates For Specified Steam Line Breaks (Contd)
II. Run 2 - 0.6 ft² Split, 30% Power, AFW Runout Protection Failure Mass Flow Rate Energy Flow Rate Time (sec) (lbm/sec) (Btu/sec)
.9920E+02 .5368E+03 .6465E+06
.1162E+03 .5149E+03 .6201E+06
.1342E+03 .4912E+03 .5916E+06
.2042E+03 .4186E+03 .5039E+06
.3042E+03 .3738E+03 .4497E+06
.4102E+03 .3229E+03 .3881E+06
.5122E+03 .2721E+03 .3265E+06
.6022E+03 .2348E+03 .2812E+06
.6242E+03 .2443E+03 .2928E+06
.7002E+03 .2300E+03 .2754E+06 Containment Functional Design 6.2.1-141
WATTS BAR WBNP-112 Table 6.2.1-39 Mass and Energy Release Rates For Specified Steam Line Breaks (Contd)
III. Run 3 - 0.35 ft² Split, 30% Power, AFW Runout Protection Failure Mass Flow Rate Energy Flow Rate Time (sec) (lbm/sec) (Btu/sec)
.1000E-01 .8057E+03 .9565E+06
.6000E+00 .8041E+03 .9548E+06
.1000E+01 .8013E+03 .9516E+06
.2000E+01 .7953E+03 .9447E+06
.3000E+01 .7897E+03 .9383E+06
.4000E+01 .7845E+03 .9324E+06
.6000E+01 .7752E+03 .9217E+06
.8000E+01 .7664E+03 .9115E+06
.1000E+02 .7736E+03 .9199E+06
.1580E+02 .7857E+03 .9338E+06
.2000E+02 .7789E+03 .9260E+06
.2220E+02 .7501E+03 .8931E+06
.2320E+02 .7358E+03 .8766E+06
.2420E+02 .7227E+03 .8615E+06
.2520E+02 .7105E+03 .8474E+06
.2670E+02 .6937E+03 .8279E+06
.2820E+02 .6783E+03 .8101E+06
.2920E+02 .6688E+03 .7990E+06
.3270E+02 .6386E+03 .7639E+06
.3570E+02 .6161E+03 .7375E+06
.3970E+02 .5900E+03 .7069E+06
.4420E+02 .5647E+03 .6771E+06
.4920E+02 .5410E+03 .6492E+06
.5570E+02 .5157E+03 .6192E+06
.6320E+02 .4917E+03 .5909E+06
.7270E+02 .4673E+03 .5618E+06
.8420E+02 .4437E+03 .5338E+06
.9920E+02 .4197E+03 .5051E+06
.1182E+03 .3969E+03 .4779E+06
.1442E+03 .3727E+03 .4489E+06 6.2.1-142 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-39 Mass and Energy Release Rates For Specified Steam Line Breaks (Contd)
III. Run 3 - 0.35 ft² Split, 30% Power, AFW Runout Protection Failure Mass Flow Rate Energy Flow Rate Time (sec) (lbm/sec) (Btu/sec)
.1792E+03 .3500E+03 .4216E+06
.2222E+03 .3254E+03 .3919E+06
.2662E+03 .3004E+03 .3619E+06
.3182E+03 .2752E+03 .3314E+06
.3782E+03 .2513E+03 .3026E+06
.4542E+03 .2277E+03 .2740E+06
.5422E+03 .2029E+03 .2439E+06
.6022E+03 .1877E+03 .2255E+06
.6382E+03 .1955E+03 .2350E+06
.7002E+03 .1904E+03 .2288E+06 Containment Functional Design 6.2.1-143
WATTS BAR WBNP-112 t
Table 6.2.1-40 Steam Line Break Cases For Core Integrity Boric Acid Concentration Case Type of Break (ppm) 1 Hypothetical with offsite power, downstream of the flow restrictor 0 2 Hypothetical without offsite power, downstream of the flow 0 restrictor 3 Credible - Uniform 0 4 Credible - Nonuniform 0 6.2.1-144 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-41 Line Break(1) Descriptions For Mass And Energy Releases 100.6% Power - AFW Pump Runout Protection Failure 100.6% Power - Feed Control Valve (FCV) Failure 100.6% Power - No Failure 100.6% Power - Feedwater Isolation Valve (FWIV) Failure 0% Power - AFW Pump Runout Protection Failure 0% Power - Feed Control Valve (FCV) Failure 0% Power - No Failure 0% Power - Feedwater Isolation Valve (FWIV) Failure Notes:
(1) For 1.4 ft2 break Containment Functional Design 6.2.1-145
WATTS BAR WBNP-112 Table 6.2.1-42 Small Break Descriptions For Mass And Energy Break Size (ft2) Description 0.944 30% Power - AFW Pump Runout Protection Failure 0.6 30% Power - AFW Pump Runout Protection Failure 0.35 30% Power - AFW Pump Runout Protection Failure 0.1 30% Power - AFW Pump Runout Protection Failure 0.86 100.6% Power - AFW Pump Runout Protection Failure 6.2.1-146 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-43 Large Break Analysis - Associated Times Maximum Lower Compartment Time, Tmax Case Temperature (°F) (sec) 1.4 ft2, 100.6% Power - AFW Pump Runout Protection Failure 323.9 53.1 1.4 ft2, 100.6% Power - FCV Failure 289.483 3.11 1.4 ft2, 100.6% Power - FWIV Failure 289.483 3.11 1.4 ft2, 100.6% Power - MSIV Failure 286.96 3.31 1.4 ft2, 0% Power - AFW Pump Runout Protection Failure 287.37 3.16 1.4 ft2, 0% Power - FCV Failure 287.30 3.21 1.4 ft2, 0% Power - FWIV Failure 287.28 3.21 1.4 ft2, 0% Power - MSIV Failure 288.28 2.51 Containment Functional Design 6.2.1-147
WATTS BAR WBNP-112 Table 6.2.1-44 Small Break Analysis - Small Split - Associated Times Maximum Lower 1
Case Compartment Time, Tmax (ft2) Temperature (°F) (sec) 0.86 325.34 83.28 0.944 325.12 80.46 0.6 325.1 112.9 0.35 324.4 191.4 0.1 317.74 646.77 1 All with AFW pump runout protection failure and 30% power, except that 0.86 ft2 break is at 100.6%
power.
6.2.1-148 Containment Functional Design
WATTS BAR WBNP-112 Table 6.2.1-45 Safety Injection Flow Minimum Safeguards Injection Mode RCS Pressure (psia) Total Flow (gpm) 15.0 4,767.77 28.2 4,594.73 55.0 4,309.98 115.0 3,456.89 175.0 2,047.63 215.0 866.15 315.0 835.40 Injection Mode (Post-Reflood Phase)
RCS Pressure (psia) Total Flow (gpm) 13.5 4,594.73 Cold Leg Recirculation Mode (w/o Residual Heat Removal [RHR] Spray)
RCS Pressure (psia) Total Flow (gpm) 0 3,093 Cold Leg Recirculation Mode (w/ RHR Spray)
RCS Pressure (psia) Total Flow (gpm) 0 794 Containment Functional Design 6.2.1-149
WATTS BAR WBNP-112 THIS PAGE INTENTIONALLY BLANK 6.2.1-150 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-1 Containment Pressure Versus Time Containment Functional Design 6.2.1-151
WATTS BAR 6.2.1-152 Containment Functional Design Figure 6.2.1-2a Upper Compartment Temperature Versus Time WBNP-112
WATTS BAR WBNP-112 Figure 6.2.1-2b Lower Compartment Temperature Versus Time Containment Functional Design 6.2.1-153
WATTS BAR WBNP-112 Figure 6.2.1-3 Active and Inactive Sump Temperature Transients 6.2.1-154 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-4 Melted Ice Mass Transient Containment Functional Design 6.2.1-155
WATTS BAR WBNP-112 Figure 6.2.1-4a Comparison of Containment Pressure Versus Ice Melt 6.2.1-156 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-5 Plan at Equipment Rooms Elevation Containment Functional Design 6.2.1-157
WATTS BAR WBNP-112 Figure 6.2.1-6 Containment Section View 6.2.1-158 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-7 Plan View at Ice Condenser Elevation Ice Condenser Compartments Containment Functional Design 6.2.1-159
WATTS BAR WBNP-112 Figure 6.2.1-8 Layout of Containment Shell Containment Functional Design 6.2.1-160
WATTS BAR WBNP-112 Figure 6.2.1-9 TMD Code Network Containment Functional Design 6.2.1-161
WATTS BAR WBNP-112 Figure 6.2.1-10 Upper and Lower Compartment Pressure Transient for Worst Case Break Compartment (Element 1) Having a DEHL Break 6.2.1-162 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-11 Upper and Lower Compartment Pressure Transient for Worst Case Break Compartment (Element 1) Having a DECL Break.
Containment Functional Design 6.2.1-163
WATTS BAR WBNP-112 Figure 6.2.1-12 Illustration of Choked Flow Characteristics 6.2.1-164 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-13 Sensitivity of Peak Pressure to Air Compression Ratio Containment Functional Design 6.2.1-165
WATTS BAR WBNP-112 Figure 6.2.1-14 Steam Concentration in a Vertical Distribution Channel 6.2.1-166 Containment Functional Design
WATTS BAR Containment Functional Design Figure 6.2.1-15 Peak Compression Pressure Versus Compression Ratio WBNP-112 6.2.1-167
WATTS BAR 6.2.1-168 Containment Functional Design WBNP-112 Figure 6.2.1-16 Peak Compartment Pressure versus Blowdown Rate
WATTS BAR WBNP-112 Figure 6.2.1-17 Sensitivity of Peak Compression Pressure to Deck Bypass Containment Functional Design 6.2.1-169
WATTS BAR WBNP-112 Figure 6.2.1-18 Pressure Increase Versus Deck Area From Deck Leakage Tests 6.2.1-170 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-19 Energy Release at Time of Compression Peak Pressure From Full-Scale Section Tests with 1-Foot Diameter Baskets Containment Functional Design 6.2.1-171
WATTS BAR WBNP-112 Figure 6.2.1-20 Pressure Increase Versus Deck Area From Deck Leakage Tests 6.2.1-172 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-21 Deleted by Amendment 97 Containment Functional Design 6.2.1-173
WATTS BAR WBNP-112 Figure 6.2.1-22 Deleted by Amendment 97 6.2.1-174 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-23 Deleted by Amendment 97 Containment Functional Design 6.2.1-175
WATTS BAR WBNP-112 Figure 6.2.1-24 Deleted by Amendment 97 6.2.1-176 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-25 Deleted by Amendment 97 Containment Functional Design 6.2.1-177
WATTS BAR WBNP-112 Figure 6.2.1-26 Deleted by Amendment 97 6.2.1-178 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-27 Containment Model Schematic.
Containment Functional Design 6.2.1-179
WATTS BAR WBNP-112 Figure 6.2.1-28 Reactor Cavity TMD Network.
6.2.1-180 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-29 Reactor Vessel Annulus Containment Functional Design 6.2.1-181
WATTS BAR WBNP-112 Figure 6.2.1-30 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-182 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-31 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-183
WATTS BAR WBNP-112 Figure 6.2.1-32 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-184 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-33 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-185
WATTS BAR WBNP-112 Figure 6.2.1-34 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-186 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-35 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-187
WATTS BAR WBNP-112 Figure 6.2.1-36 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-188 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-37 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-189
WATTS BAR WBNP-112 Figure 6.2.1-38 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-190 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-39 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-191
WATTS BAR WBNP-112 Figure 6.2.1-40 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-192 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-41 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-193
WATTS BAR WBNP-112 Figure 6.2.1-42 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-194 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-43 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-195
WATTS BAR WBNP-112 Figure 6.2.1-44 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-196 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-45 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-197
WATTS BAR WBNP-112 Figure 6.2.1-46 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-198 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-47 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-199
WATTS BAR WBNP-112 Figure 6.2.1-48 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-200 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-49 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-201
WATTS BAR WBNP-112 Figure 6.2.1-50 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-202 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-51 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-203
WATTS BAR WBNP-112 Figure 6.2.1-52 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-204 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-53 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-205
WATTS BAR WBNP-112 Figure 6.2.1-54 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-206 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-55 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-207
WATTS BAR WBNP-112 Figure 6.2.1-56 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-208 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-57 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-209
WATTS BAR WBNP-112 Figure 6.2.1-58 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-210 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-59 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-211
WATTS BAR WBNP-112 Figure 6.2.1-60 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-212 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-61 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-213
WATTS BAR WBNP-112 Figure 6.2.1-62 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-214 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-63 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-215
WATTS BAR WBNP-112 Figure 6.2.1-64 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-216 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-65 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-217
WATTS BAR WBNP-112 Figure 6.2.1-66 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-218 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-67 127 Square Inch Cold Leg Break (Reactor Cavity Analysis)
Containment Functional Design 6.2.1-219
WATTS BAR WBNP-112 Figure 6.2.1-68 127 Square Inch Cold Leg Break (Reactor Cavity Analysis) 6.2.1-220 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-69 Compartment Temperature 1.4 ft2/Loop, 100.6% Power AFW Runout Protection Failure Containment Functional Design 6.2.1-221
WATTS BAR WBNP-112 Figure 6.2.1-70 Lower Compartment Pressure 1.4 ft2 Loop, 100.6% Power AFW Runout Protection Failure 6.2.1-222 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-71 Compartment Temperature 0.35 ft2 Split, 30% Power AFW Runout Protection Failure Containment Functional Design 6.2.1-223
WATTS BAR WBNP-112 Figure 6.2.1-72 Lower Compartment Pressure 0.35 ft2 Split, 30% Power AFW Runout Protection Failure 6.2.1-224 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-73 Compartment Temperature 0.6 ft2 Split, 30% Power AFW Runout Protection Failure Containment Functional Design 6.2.1-225
WATTS BAR WBNP-112 Figure 6.2.1-74 Lower Compartment Pressure 0.6 ft2 Split, 30% Power AFW Runout Protection Failure 6.2.1-226 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-75 Maximum Reverse Pressure Differential Model Containment Functional Design 6.2.1-227
6.2.1-228 WATTS BAR Figure 6.2.1-76 Maximum Reverse Pressure Differential Upper and Lower Compartment Pressures WBNP-112 Containment Functional Design
WATTS BAR Containment Functional Design Figure 6.2.1-77 Maximum Reverse Pressure Differential Upper and Lower Compartment Temperatures WBNP-112 6.2.1-229
6.2.1-230 WATTS BAR Figure 6.2.1-78 Maximum Reverse Pressure Differential Upper to Lower Compartment Flowrates WBNP-112 Containment Functional Design
WATTS BAR Containment Functional Design Figure 6.2.1-79 Maximum Reverse Pressure Differential Case 6 Upper and Lower Compartment Pressures WBNP-112 6.2.1-231
6.2.1-232 WATTS BAR Figure 6.2.1-80 Maximum Reverse Pressure Differential Case 6 Upper and Lower Compartment Temperatures WBNP-112 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-81 Steam Generator Enclosure Nodalization Containment Functional Design 6.2.1-233
6.2.1-234 WATTS BAR Figure 6.2.1-82 Flow Paths For TMD Steam Generator Enclosure Short-term Pressure Analysis WBNP-112 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-83 Pressure Transient Between Break Element And Upper Compartment (Steam Generator Enclosure Analysis)
Containment Functional Design 6.2.1-235
WATTS BAR WBNP-112 Figure 6.2.1-84 Differential Pressure Transient Across The Steam Generator Vessel (Steam Generator Enclosure Analysis) 6.2.1-236 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-85 Differential Pressure Transient Across The Steam Generator Vessel (Steam Generator Enclosure Analysis)
Containment Functional Design 6.2.1-237
WATTS BAR WBNP-112 Figure 6.2.1-86 Pressure Versus Time For The Break Element (Steam Generator Enclosure Analysis) 6.2.1-238 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-86a Upper Compartment Pressure Versus Time (Steam Generator Enclosure Analysis)
Containment Functional Design 6.2.1-239
WATTS BAR WBNP-112 Figure 6.2.1-87 Nodalization Pressure Enclosure Analysis 6.2.1-240 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-88 Pressure Transient Between Break Element And Upper Compartment (Pressurizer Enclosure Analysis)
Containment Functional Design 6.2.1-241
WATTS BAR WBNP-112 Figure 6.2.1-89 Pressure Differential Across The Pressurizer Vessel (Pressurizer Enclosure Analysis) 6.2.1-242 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-90 Pressure Differential Across The Pressurizer Vessel (Pressurizer Enclosure Analysis)
Containment Functional Design 6.2.1-243
WATTS BAR WBNP-112 Figure 6.2.1-91 Pressure Differential Across The Pressurizer Vessel (Pressurizer Enclosure Analysis) 6.2.1-244 Containment Functional Design
WATTS BAR WBNP-112 Figure 6.2.1-92 Pressure Versus Time For The Break Element (Pressurizer Enclosure Analysis)
Containment Functional Design 6.2.1-245
WATTS BAR WBNP-112 THIS PAGE INTENTIONALLY BLANK 6.2.1-246 Containment Functional Design
WATTS BAR WBNP-112 6.2.2 CONTAINMENT HEAT REMOVAL SYSTEMS Adequate containment heat removal capability for the ice condenser reactor containment is provided by the ice condenser (Section 6.7), the air return fan system (Section 6.8), and two separate containment heat removal spray systems whose components operate in the sequential modes described in Section 6.2.2.2. One of these heat removal spray systems is the containment spray system, and the second is the residual heat removal spray system, which is a portion of the residual heat removal system (Section 6.3).
Minimum engineered safety feature performance of the containment heat removal systems is achieved with the following:
(1) Ice condenser (Section 6.7)
(2) One train of the air return fan system (3) One train of the containment spray system (4) One train of the residual heat removal spray system (not required for steam or feed line break)
Each spray system consists of two trains of redundant equipment per reactor unit.
There are four spray headers per unit. Two headers are supplied from separate trains of the containment spray system; the other two are supplied by separate trains of the RHR spray system. Each individual train consists of a pump, a heat exchanger, appropriate control valves, required piping, and a header with nozzles located in the upper compartment of the containment with flow directed to obtain full coverage of the containment upper volume during an emergency. The systems use borated water supplied from the refueling water storage tank and/or the recirculation sump.
6.2.2.1 Design Bases The primary design basis for the containment heat removal spray systems is to spray cool water into the containment atmosphere when appropriate in the event of a loss-of-coolant accident or secondary side break and thereby ensure that the containment pressure cannot exceed the containment shell maximum internal pressure of 15.0 psig at 250°F, which corresponds to the code design internal pressure of 13.5 psig at 250°F (see Section 3.8.2). This protection is afforded for all pipe break sizes up to and including the hypothetical instantaneous circumferential rupture of the reactor coolant loop resulting in unobstructed flow from both pipe ends. After the ice has melted, the containment spray system and the residual heat removal spray system become the sole systems for removing energy directly from the containment. The containment heat removal systems are designed to provide a means of removing containment heat without loss of functional performance in the post-accident containment environment and operate without benefit of maintenance for the duration of time to restore and maintain containment conditions at atmospheric pressure. Although the water in the core after a loss-of-coolant accident is quickly subcooled by the emergency core cooling system (Section 6.3), the design of heat removal capability of each CONTAINMENT HEAT REMOVAL SYSTEMS 6.2.2-1
WATTS BAR WBNP-112 containment heat removal system is based on the conservative assumption that the core residual heat is released to the containment as steam which eventually melts all ice in the ice condenser.
The containment spray system provides two redundant heat removal trains. The system is designed such that both trains are automatically started by high-high containment pressure signal. The signal actuates, as required, all controls for positioning all valves to their operating position and starts the pumps. The operator can also manually actuate the entire system from the control room. Either of the two trains containing a pump, heat exchanger, and associated valving and spray headers is independently capable of delivering a minimum flowrate of 4,000 gpm.
The containment heat removal spray systems are designed to withstand the design basis earthquake and the operational basis earthquake without loss of function. They satisfy the TVA Class B Mechanical Requirements. The heat exchanger tube side (CSS) meets TVA Class B and the shell side (ERCW) meets TVA Class C mechanical requirements. The containment heat removal spray systems maintain their integrity and do not suffer loss of ability to perform their minimum required function due to normal operation, faults of moderate frequency, infrequent faults, and limiting faults.
Sufficient redundancy for all supporting systems necessary for minimum operational requirements of the containment heat removal spray systems is provided and complies with the single failure criteria for engineered safety features. Separate divisions on essential raw cooling water supply, power equipment heat exchangers, pumps, valves, and instrumentation are provided in order to have two completely separated trains.
The system is provided with overpressure protection from excessive pressures that could otherwise result from temperature changes, interconnection with other systems operating at higher pressures, or other means.
Those portions of the containment heat removal spray systems located outside of the containment which are designed to circulate, during post-accident conditions, radioactively contaminated water collected in the containment meet the following requirements:
(1) Shielding within guidelines of 10 CFR 20 and 10 CFR 100.
(2) Collection of discharges from pressure relieving devices.
(3) Remote means for isolating any sections under anticipated malfunction or failure conditions.
(4) Means to detect and control radioactivity leakage into the environs to limits consistent with guidelines set forth in 10 CFR 20 and 10 CFR 100.
During accident conditions, cooling of the containment spaces is provided by the ice condenser system, containment heat removal spray systems, and the air return system. In addition, during non-LOCA accidents, the lower compartment cooler (LCC) fans are utilized to recirculate air throughout the lower containment spaces to prevent 6.2.2-2 CONTAINMENT HEAT REMOVAL SYSTEMS
WATTS BAR WBNP-112 hot pockets from developing. The LCC units may be operated continuously throughout all accidents, except a MSLB, which do not initiate a containment Phase B isolation signal. After a MSLB all four coolers (2 Train A and 2 Train B) are started although only 2 are required, within 11/2 hours to 4 hours4.62963e-5 days <br />0.00111 hours <br />6.613757e-6 weeks <br />1.522e-6 months <br /> after the MSLB to recirculate air throughout the lower containment spaces, to prevent hot spots from developing. During or after a LOCA, the LCC units, including their fans, are not required to be operable.
6.2.2.2 System Design The containment spray systems consist of two separate trains of equal capacity with each train independently capable of meeting system requirements. This system can be supplemented with two residual heat removal system pumps and two residual heat exchangers in parallel, with associated piping, valves and individual spray headers in the upper containment volume. Each train includes a pump, heat exchanger, ring header with nozzles, isolation valves and associated piping, and instrumentation and controls. Partial flow from an RHR system pump through its associated heat exchanger can be used to supplement each train. Independent electrical power supplies are provided for equipment in each containment spray train. In addition each train is provided with electrical power from separate emergency diesel generators in the event of a loss of offsite electrical power. During normal operation, all of the equipment is idle and the associated isolation valves are closed.
Upon system activation during a LOCA or other high energy line break, adequate containment cooling is provided by the containment spray systems whose components operate in sequential modes. These modes are: 1) spraying a portion of the contents of the refueling water storage tank into the containment atmosphere using the containment spray pumps; 2) after the refueling water storage tank has been drained, but while there is still ice remaining in the ice condenser, recirculation of water from the containment sump through the containment spray pumps, through the containment spray heat exchangers, and back to the containment (This spray is useful in reducing sump water temperatures.); 3) diversion of a portion of the recirculation flow from the residual heat removal system to additional spray headers. RHR spray operation is initiated manually by the operator only if the emergency core cooling system and containment spray system are both operating in the recirculation mode. If switchover to recirculation occurs prior to 1 hour1.157407e-5 days <br />2.777778e-4 hours <br />1.653439e-6 weeks <br />3.805e-7 months <br /> after initiation of the LOCA, RHR spray operation can be commenced 1 hour1.157407e-5 days <br />2.777778e-4 hours <br />1.653439e-6 weeks <br />3.805e-7 months <br /> after initiation of the LOCA. If switchover to recirculation occurs later than 1 hour1.157407e-5 days <br />2.777778e-4 hours <br />1.653439e-6 weeks <br />3.805e-7 months <br /> after initiation of the LOCA, RHR spray operation can be commenced after completion of the switchover procedure.
The spray water from the containment and RHR spray systems returns from the upper compartment to the lower compartment through two 14 inch drains in the bottom of the refueling canal. The curbing around the personnel access door and the equipment access hatch on the operating deck directs spray water flow towards the refueling canal. The air-water mixture entering the air return fans will be rerouted inside the polar crane wall through the accumulator rooms utilizing curbing, the floor hatch cover and floor drainage system.
The flow diagram for this system is presented in Figure 6.2.2-1.
CONTAINMENT HEAT REMOVAL SYSTEMS 6.2.2-3
WATTS BAR WBNP-112 Component Description Pumps The containment spray system flow is provided by two centrifugal type pumps driven by electric motors. The motors, which can be powered either normally or from an emergency source are direct coupled and non-overloading to the end of the pump curve. The design head of the containment spray pump is sufficient to ensure rated capacity with a minimum level in the refueling water storage tank or the containment sump when pumping against a head equivalent to the sum of the maximum pressure of the containment post LOCA/HELB, the elevational head between the pump discharge and the uppermost spray nozzles, and the equipment and piping friction losses. Each pump is rated for 4000 gpm flow at a design head of 435 ft. See Table 6.2.2-1 for additional design parameters and Figure 6.2.2-2 for characteristic curves.
The residual heat removal pumps which also provide flow to the containment heat removal spray system are described in Section 5.5.7.2.1 and Table 5.5-8.
Each residual heat removal pump provides a design flow of 2000 (1475 gpm analytical) for upper containment spray.
Each containment spray pump is powered by a horizontal squirrel cage induction motor. Pump motor parameters are presented in Table 6.2.2-1.
Net Positive Suction Head (NPSH)
The plant and piping layout of the containment spray system ensures that the pump NPSH requirements are met at maximum runout conditions with the containment spray pumps taking suction from either the refueling water storage tank or the containment sump. The NPSH available from the containment sump is calculated using the maximum credible sump water temperature (190°F) with no credit taken for containment overpressure or height of water above the RHR Strainer Assembly.
Available NPSH parameters are given in Table 6.3-12.
Heat Exchangers The containment spray heat exchangers are the vertical counter flow U-tube type with tubes welded to the tube sheet. Borated water from either the refueling water storage tank or the containment sump circulates through the tube side. Design parameters are presented in Table 6.2.2-2.
Piping All containment heat removal spray system piping in contact with borated water is austenitic stainless steel. All piping joints are welded except for the flanged connection at the pump or where disassembly of the joint may be required.
Spray Nozzles and Ring Headers Each containment spray ring header provides 4000 gpm minimum and contains 263 hollow cone ramp bottom nozzles, each of which is capable of a design flow of 15.2 6.2.2-4 CONTAINMENT HEAT REMOVAL SYSTEMS
WATTS BAR WBNP-112 gpm with a 40 psi differential pressure. These nozzles have an approximately 3/8-inch diameter spray orifice and are not subject to clogging by particles less than 1/4 inch in maximum dimension. The nozzles produce a drop size spectrum with a median diameter of less than 700 microns at 40 psid. The spray solution is completely stable and soluble at all temperatures of interest in the containment and, therefore, does not precipitate or otherwise interfere with nozzle performance. Each nozzle header is independently oriented to maximize coverage of the containment volume inside the crane wall. This arrangement prohibits any flow into the ice condenser.
The residual heat removal spray ring headers contain 146 nozzles per header and deliver a design flow of 2000 gpm (1475 gpm analytical) per header. Each RHR spray header will perform its required design function with 142 unobstructed spray nozzles.
They have the same design characteristics as the headers in the containment spray system.
Refueling Water Storage Tank During the injection phase immediately following a LOCA or HELB, the containment spray is supplied from the refueling water storage tank.
Recirculation Sump The recirculation sump is described in Section 6.3.2.2 under the discussion of the recirculation mode.
Material Compatibility All parts of the containment spray system in contact with borated water are austenitic stainless steel or equivalent corrosion resistant material.
6.2.2.3 Design Evaluation Performance of the containment heat removal system is evaluated through analyses of the design basis accident and various other cases described in Chapter 15 and Section 6.2.1. The analyses were performed using the LOTIC code and show that the containment heat removal systems are capable of keeping the containment pressure below the containment maximum internal pressure of 15 psig, which corresponds to the code design internal pressure of 13.5 psig at 250°F (see Section 3.8.2) even when it is assumed that the minimum engineered safety features are operating. Section 6.2.1 presents a description of the analytical methods and models which were used along with verification of pertinent items from Waltz Mill tests, and curves showing the calculated performance of important variables following the design-basis loss-of-coolant accident.
The design basis accident analysis (Section 6.2.1.3.3) results in a required containment spray flow rate of 4000 gpm using 88°F** constant temperature essential raw cooling water for the heat exchangers.
1 **Note: The containment analysis was run at ERCW temperature of 88°F although the containment spray, component cooling, and residual heat removal Hx UA values are based on ERCW temperature of 85°F to provide additional conservatism.
CONTAINMENT HEAT REMOVAL SYSTEMS 6.2.2-5
WATTS BAR WBNP-112 The containment spray systems provide two full-capacity heat removal systems for the containment, each of which is sized as described in Section 6.2.2.1 to remove heat at a rate which precludes an increase of the containment maximum internal pressure above 15.0 psig, which corresponds to the code design internal pressure of 13.5 psig at 250°F (see Section 3.8.2). All spray headers and spray nozzles are located inside the containment in the upper compartment and can withstand, without loss of function or maintenance, the post-accident containment environment. The remainder of the systems, with the exception of the refueling water storage tanks, which includes all active components, are located in the Auxiliary Building and, therefore, are not affected by wind, tornado, or snow and ice conditions.
The design is based on the spray water being raised to the saturation temperature of the containment in falling through the steam-air mixture within the building. The minimum fall path of the droplets is approximately 75 ft from the spray ring headers to the operating deck. The actual fall path is longer due to the trajectory of the droplets sprayed out from the ring header nozzles. Figures 6.2.2-3 through 6.2.2-6 depict the containment spray coverage for the containment spray system.
Except for the refueling water storage tank water supplied by the safety injection system, the containment spray system initially operates independently of other engineered safety features. For extended operation in the recirculation mode, water is supplied to the containment RHR spray headers through the residual heat removal pumps and residual heat removal exchangers. One containment spray system train, supplemented by one RHR spray train, when required, provides adequate heat removal capability to limit containment pressure below design (see Section 6.2.1.3).
RHR spray is required only after switchover to the recirculation mode and no earlier than 1 hour1.157407e-5 days <br />2.777778e-4 hours <br />1.653439e-6 weeks <br />3.805e-7 months <br /> after initiation of the LOCA. At this time one RHR pump can provide sufficient RHR spray as well as adequate core flow via the high head (one centrifugal charging and one safety injection) pumps. (See Section 6.3.3 for the performance evaluation of the RHR pumps in their core cooling function.)
All active components of the system were analyzed to show that the failure of any single active component does not prevent fulfilling the design function. This analysis is summarized in Table 6.2.2-3. A single failure in the residual heat removal system will not prevent long-term use of the spray system. The analyses of the loss-of-coolant accident presented in Chapter 15 reflect the single failure analysis. Each of the spray trains provides complete backup for the other.
An analysis of the spray return drains located in the refueling canal has been made to show that they are adequately sized for a maximum RHR and containment spray flow and ensures an adequate water supply in the lower compartment to satisfy pump NPSH requirements.
The passive portions of the spray systems located within the containment are designed to withstand, without loss of functional performance, a post accident containment environment and to operate without benefit of maintenance.
6.2.2-6 CONTAINMENT HEAT REMOVAL SYSTEMS
WATTS BAR WBNP-112 The spray headers which are located in the upper containment volume are separated from the reactor and primary coolant loops by the operating deck and inner wall of the ice bed. These spray headers are therefore protected from missiles originating in the lower compartment.
This evaluation shows that the containment spray systems can withstand expected conditions during the 40-year life of the plant without loss of capability to perform the required safety functions. Specifically, the system achieved this by having been designed to meet applicable General Design Criteria (GDC) as follows:
(1) The systems can withstand the effects of natural phenomena as required by GDC 2.
(2) The systems are designed to accommodate the effects of and be compatible with the environmental conditions associated with normal operation, maintenance, testing, and postulated accidents including loss of coolant as required by GDC 4.
(3) The systems are not shared with another nuclear power unit as required by GDC 5.
(4) The systems are designed to be capable of being inspected and tested to ensure reliability throughout their life as required by GDC 39 and 40.
(5) The systems are designed adequately to provide post-accident cooling inside the primary containment to reduce the containment pressure and temperature following any LOCA and maintain them at acceptable levels, as required by GDC 38.
(6) The systems are designed to aid in the control and removal of fission products, hydrogen, oxygen, and other substances which may be released into the reactor containment following postulated accidents to assure that containment integrity is maintained, as required by GDC 41.
Tritium Production Core Evaluation (Unit 1 Only)
The effects of converting WBN to a Tritium Production Core (TPC) on the containment heat removal systems have been evaluated. The evaluation includes the effect of adding a leading edge flow meter (LEFM) into the main feedwater piping and the effect of uprating the plant nominal power level by 1.4%.
Based on the conclusions in Section 6.2.3.12 that mass and energy releases for LOCA and secondary side pipe ruptures do not have an adverse impact on the primary containment functionality due to incorporation of a TPC, the containment heat removal system will not be impacted.
6.2.2.4 Testing and Inspections Performance tests of the active components in the system are performed in the manufacturer's plant and followed by in-place preoperational testing.
CONTAINMENT HEAT REMOVAL SYSTEMS 6.2.2-7
WATTS BAR WBNP-112 Capability is provided to test initially and subsequently on a routine basis to the extent practical the operational startup sequence and performance capability of the containment spray system including the transfer to alternate power sources.
Capability to test periodically the delivery capacity of the containment spray system at a position as close to the spray header as is practical and for obstruction of the spray nozzles is provided. As part of the preoperational test program, the containment spray nozzles are physically verified to pass an unobstructed flow of air. The air is introduced into the headers through an air test connection on each header.
Initially, the containment spray system is hydrostatically tested to the applicable code test pressure.
All periodic tests of individual components or the complete containment spray system are controlled to ensure that plant safety is not jeopardized and that undesirable transients do not occur.
The containment spray system is designed to comply with ASME Section XI, "Inservice Inspection of Nuclear Reactor Coolant System." Detailed test procedures are given in Chapter 14.
6.2.2.5 Instrumentation Requirements The containment spray system is actuated either manually from the control room or external to the main control room or automatically by the coincidence of two sets out of four protection set loops monitoring the lower containment pressure. The high-high containment pressure signal starts the containment spray pumps and positions all valves to their operating configuration.
The operation of the containment spray system is verified by instrument readout in the control room. Pump motor breakers energize indicating lights on the control panel to show power is being supplied to the pump motors. Status lights on the main control panel indicate valve position and are energized independently of the valve actuation signal.
To protect the pumps from low flow conditions, a mini-flow recirculation line is provided to allow pump discharge to be circulated back into the pump suction line. This line is opened by a motor-operated valve when flow in the discharge line drops below that required for pump protection or if, upon starting, flow is not achieved in the spray header within a preset time interval. Elbow taps in each discharge line provide a delta-p measurement to monitor the flow rate and provide the flow signal for the control room flow indicators and to control the minimum flow recirculation valve.
Local instruments monitor the following parameters: containment spray pump suction and discharge pressure, heat exchanger inlet temperature, heat exchanger inlet and outlet pressure, and containment spray test line flow.
In the event of a main control room evacuation, the necessary control functions are transferable to outside of the main control room in order to assure that the system can be aligned and locked to prevent inadvertent operation and to manually initiate system 6.2.2-8 CONTAINMENT HEAT REMOVAL SYSTEMS
WATTS BAR WBNP-112 operation if necessary. The control transfer is provided for the spray pumps, containment spray isolation valves, and containment sump isolation valves.
The system is designed as Seismic Category I. The instrumentation and associated interconnected wiring and cables are physically and otherwise separated so that a single event cannot cause malfunction of the entire system.
6.2.2.6 Materials All parts of the containment spray system in contact with borated water are austenitic stainless steel or equivalent corrosion-resistant material. None of these materials produce radiolytic or pyrolytic decomposition products that can interfere with this or other engineered safety features.
CONTAINMENT HEAT REMOVAL SYSTEMS 6.2.2-9
WATTS BAR WBNP-112 Table 6.2.2-1 Containment Spray Pump/Motor Design Parameters Pump Quantity Per Unit 2 Design Pressure, psig 300 Design Temperature, °F 250 Design Flow Rate, gpm 4000 Design Head, ft 435 Motor Horsepower, hp 700 Service Factor 1.15 Voltage, V 6600 Phase 3 Cycles, Hz 60 6.2.2-10 CONTAINMENT HEAT REMOVAL SYSTEMS
WATTS BAR WBNP-112 Table 6.2.2-2 Containment Spray Heat Exchanger Design Parameters Quantity Per Unit 2 Type Counter Flow Percent Tubes Plugged 10%
Heat Transfer Per Unit, Btu/hr 12.85 x 107 Shell-Side Flow, gpm 5,200 Tube-Side Flow, gpm 4,000 Tube-Side Inlet Temperature, °F 190 Shell-Side Inlet Temperature, °F 85 Tube-Side Outlet Temperature, °F 124.7 Shell-Side Outlet Temperature, °F 129.5 Design Pressure (Shell/Tube), psig 150/300 Design Temperature (Shell/Tube), °F 200/250 Heat Exchanger UA, Btu/hr-°F 2.44 x 106 CONTAINMENT HEAT REMOVAL SYSTEMS 6.2.2-11
6.2.2-12 Table 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS (Page 1 of 8)
ITEM FAILURE POTENTIAL METHOD OF EFFECTS ON EFFECT ON NO.COMPONENT FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS WATTS BAR INJECTION MODE
- 1. Containment To pump borated Fails to start Mechanical Indication via CS System None. Two Only one train is Spray Pump A-A water to spray failure or switches HS-72-27A Train "A" is lost 100% capacity required to nozzles in the electrical & -27C trains are mitigate accident containment failure due to provided. consequences.
loss of power
- 2. Containment Spray To pump borated Fails to start Mechanical Indication via CS System None. Two Only one train is Pump B-B water to spray failure or switches HS-72-10A Train "B" is lost 100% capacity required to nozzles in the electrical & -10C trains are mitigate accident containment failure due to provided. consequences.
loss of power
- 3. Valve FCV 72-21 Provide water flow Fails closed Mechanical Valve position CS System None. CS Only one train is path to CS PMP B-B failure indication via switch Train "B" is System Train required to blockage or HS-72-21A inoperable "A" is used to mitigate accident spurious supply water consequences.
electrical signal to nozzles
- 4. Valve FCV 72-22 Provide water flow Fails Closed Mechanical Valve position CS System None. CS Only one train is path to CS PMP A-A failure indication via switch Train "A" is System train required to blockage or HS-72-22A inoperable "B" is used to mitigate accident spurious supply water consequences.
electrical signal to nozzles CONTAINMENT HEAT REMOVAL SYSTEMS WBNP-112
Table 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS (Page 2 of 8)
ITEM FAILURE POTENTIAL METHOD OF EFFECTS ON EFFECT ON NO.COMPONENT FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS WATTS BAR
- 5. Valve FCV 72-02 Water flow path to Fails to open Mechanical Valve position CS System None. Two Only one train is containment spray failure or loss indication via Train "B" is lost 100% capacity required to nozzles of power to switches trains are mitigate accident valve motor HS-72-2A/ provided. consequences.
HS-72-2B*
Recloses Mechanical Valve position CS System None. Two Only one train is CONTAINMENT HEAT REMOVAL SYSTEMS after opening failure or indication via Train "B" is lost 100% capacity required to spurious switches trains are mitigate accident electrical signal HS-72-2A/HS-72-2B provided. consequences.
- 6. Valve FCV 72-039 Water flow path to Fails to open Mechanical Valve position CS System None. Two Only one train is containment spray failure or loss indication via Train "A" is lost 100% capacity required to nozzles of power to switches trains are mitigate accident valve motor HS-72-39A/ provided. consequences.
HS-72-39B Recloses Mechanical Valve position CS System None. Two Only one train is after opening failure or indication via Train "A" is lost 100% capacity required to spurious switches trains are mitigate accident electrical signal HS-72-39A/ provided. consequences.
HS-72-39B
- 7. Emergency power Provide power to Fails Diesel Voltmeters in CS System None. Two Only one train is to Train A PMP A motor & all generator Control Room Train "A" is lost 100% capacity required to MOVs in Train A shutdown Bd. trains are mitigate accident 1A-A failure provided. consequences.
- Note: Valve position indication for Valve FCV-72-02 may be derived from indicator lights on all three hand switches (HS-72-2A, HS-72-2B or HS-72-2C). This is unique in that 2B hand switches have been removed from nearly all other applied uses due to EQ considerations.
6.2.2-13 WBNP-112
Table 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS 6.2.2-14 (Page 3 of 8)
ITEM FAILURE POTENTIAL METHOD OF EFFECTS ON EFFECT ON NO.COMPONENT FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS WATTS BAR
- 8. Emergency Power Provide power to Fails Diesel Voltmeters in CS System None. Two Only one train is to Train B PMP B motor & all generator Control Room Train "B" is lost 100% capacity required to MOVs in Train B shutdown Bd. trains are mitigate accident 1B-B failure provided. consequences.
- 9. FCV-72-34 Isolate pump A-A Fails open Mechanical Valve position Water flowing Train "A" Only one train is discharge from failure or indication via switch into spray capability required to suction spurious HS-72-34A nozzles will be reduced. No mitigate accident electrical signal diminished. impact on consequences.
plant; operator can put 100%
train B in operation.
- 10. FCV-72-13 Isolate pump B-B Fails open Mechanical Valve position Water flowing Train "B" Only one train is discharge from failure or indication via switch into spray capability required to suction spurious HS-72-13A nozzles will be reduced. No mitigate accident electrical signal reduced. impact on consequences.
plant; operator can put 100%
train A in operation.
- 11. Check VA.72-506 Flow path to CS Valve stuck Mechanical Pump discharge Train A is None. Two Pump A-A closed failure flow indicator inoperable 100%
FI-72-34 capability trains are provided.
CONTAINMENT HEAT REMOVAL SYSTEMS WBNP-112
Table 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS (Page 4 of 8)
ITEM FAILURE POTENTIAL METHOD OF EFFECTS ON EFFECT ON NO.COMPONENT FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS WATTS BAR
- 12. Check VA 72-507 Flow path to CS Valve stuck Mechanical Pump discharge Train B is None. Two Pump B-B closed failure flow indicator inoperable 100%
FI-72-13 capability trains are provided.
- 13. Check VA 72-524 CS Pump A-A Valve stuck Mechanical Flow measurement Train A is None. Two CONTAINMENT HEAT REMOVAL SYSTEMS discharge flow path closed failure via flow indicator inoperable 100%
FI-72-34 capability trains are provided.
- 14. Check VA 72-525 CS Pump B-B Valve stuck Mechanical Flow measurement Train B is None. Two discharge flow path closed failure via flow indicator inoperable 100%
FI-72-13 capability trains are provided.
- 15. Check VA 72-548 Flow path to Train A Valve stuck Mechanical Pump discharge via Train A is None. Two spray nozzles closed failure flow indicator inoperable 100%
FI-72-34 capability trains are provided.
- 16. Check VA 72-549 Flow path to Train B Valve stuck Mechanical Pump discharge via Train B is None. Two spray nozzles closed failure flow indicator inoperable 100%
FI-72-13 capability trains are provided.
6.2.2-15 WBNP-112
Table 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS 6.2.2-16 (Page 5 of 8)
ITEM FAILURE POTENTIAL METHOD OF EFFECTS ON EFFECT ON NO.COMPONENT FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS WATTS BAR
- 17. Relief VA 72-508 CS Pump A-A Valve fails Mechanical Train A capacity None. Two suction piping over- open failure will be 100% capacity pressure protection diminished trains provided.
- 18. Relief VA 72-509 CS Pump B-B Valve fails Mechanical Train B capacity None. Two suction piping over- open failure will be 100% capacity pressure protection diminished trains provided.
RECIRC. MODE ACTIVE FAILURE
- 19. Valve FCV-72-44 Train A flow path Fails to open Mechanical Valve position Train "A" is None. Two from containment or recloses failure or indication via inoperable 100% capacity sump after opening electrical switches trains are failure HS-72-44A, provided.
HS-72-44B, HS-72-44C 20 Valve FCV-72-45 Train B flow path Fails to open Mechanical Valve position Train "B" is None. Two from containment or recloses failure or indication via inoperable 100% capacity sump after opening electrical switches trains are failure HS-72-45A, provided.
HS-72-45B, HS-72-45C CONTAINMENT HEAT REMOVAL SYSTEMS WBNP-112
Table 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS (Page 6 of 8)
ITEM FAILURE POTENTIAL METHOD OF EFFECTS ON EFFECT ON NO.COMPONENT FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS WATTS BAR
- 21. Valve FCV-72-22 Isolate "RWST" Fails to close Mechanical Valve position Train "A" is None. Two Interlock will during recirc. mode failure or indication via switch inoperable 100% capacity prevent opening electrical HS-72-22A trains are of FCV-72-44.
failure provided.
- 22. Valve FCV-72-21 Isolate "RWST" Fails to close Mechanical Valve position Train "B" is None. Two Interlock will CONTAINMENT HEAT REMOVAL SYSTEMS during recirc. mode failure or indication via switch inoperable 100% capacity prevent opening electrical HS-72-21A trains are of FCV-72-45.
failure provided.
Spray Heat spray water lost system temp. indication via Train A can not capacity Train Exch. A mechanical or ICS point T0168A be cooled. B will be electrical operated.
failure
Spray Heat spray water lost system temp. indication via Train B can not capacity Train Exch. B mechanical or ICS point T0169A. be cooled. A will be electrical operated.
failure
during recirc. mode open failure FCV-72-22 will isolate RWST.
during recirc. mode open failure FCV-72-21 will isolate RWST.
6.2.2-17 WBNP-112
Table 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS 6.2.2-18 (Page 7 of 8)
ITEM FAILURE POTENTIAL METHOD OF EFFECTS ON EFFECT ON NO.COMPONENT FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS WATTS BAR PASSIVE
- 27. Containment Cools CS water Clogging/ Impurities, High CS water Diminished heat None. Two Only one train is Spray Heat during recirc. mode tube rupture particulate Temp. indication via transfer 100% capacity required to Exch. A matter ICS point T0168A capability in trains mitigate accident Train A including heat consequences.
exchangers are provided.
- 28. Containment Cools CS water Clogging/ Impurities, High CS water Diminished heat None. Two Only one train is Spray Heat during recirc. mode tube rupture particulate Temp. indication via transfer 100% capacity required to Exch. B matter ICS point T0169A. capability in trains mitigate accident Train B including heat consequences.
exchangers are provided.
- 29. Spray nozzles Spray water in the Clogged Impurities, Reduced pump flow 263 nozzles Redundant Nozzles are 3/8 containment particulate provided per trains are inch diameter matter. CSS train. Will provided to and Containment diminish cooling fulfill minimum Sump strainer capacity slightly. plant perforation size requirements. is 0.085 inch, so possibility of clogging is remote.
- 30. Piping or valve Ruptures or In service Inspection System None. Two Only one train is body or pump major capability 100% capacity required to casing or HX, leakage diminished. trains are mitigate accident shell provided. consequences.
CONTAINMENT HEAT REMOVAL SYSTEMS WBNP-112
Table 6.2.2-3 FAILURE MODES AND EFFECTS ANALYSIS (Page 8 of 8)
ITEM FAILURE POTENTIAL METHOD OF EFFECTS ON EFFECT ON NO.COMPONENT FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS WATTS BAR
- 31. All valves Disc Mechanical System None. Two required for separated failure capability 100% capacity system operation from stem diminished trains are provided.
CONTAINMENT HEAT REMOVAL SYSTEMS 6.2.2-19 WBNP-112
WATTS BAR WBNP-112 THIS PAGE INTENTIONALLY LEFT BLANK 6.2.2-20 CONTAINMENT HEAT REMOVAL SYSTEMS
WATTS BAR Containment Heat Removal Systems Figure 6.2.2-1 Powerhouse Units 1 & 2 Mechanical Flow Diagram Containment Spray System WBNP-112 6.2.2-21
WATTS BAR WBNP-112 Figure 6.2.2-2 Containment Spray Pump Performance Curves Containment Heat Removal Systems 6.2.2-22
WATTS BAR Containment Heat Removal Systems Figure 6.2.2-3 Reactor Bldgs. Units 1 & 2 Mechanical Containment Spray System 6.2.2-23 Piping Plan of Spray Patterns From C.S. Loop Header A WBNP-112
[Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.2-4 Powerhouse-Auxiliary & Reactor Bldgs Units 1 & 2 Mechanical Containment Spray System Piping Containment Heat Removal Systems 6.2.2-24
WATTS BAR Containment Heat Removal Systems Figure 6.2.2-5 Reactor Bldgs. Units 1 & 2 Mechanical Containment Spray System Piping 6.2.2-25 Plan of Spray Patterns From C.S. Loop Header B WBNP-112
WATTS BAR Containment Heat Removal Systems Figure 6.2.2-6 Reactor Bldgs. Units 1 & 2 Mechanical Containment Spray System Piping Section of Spray Patterns From C.S. Loop Header B WBNP-112 6.2.2-26
WATTS BAR WBNP-112 6.2.3 Secondary Containment Functional Design Structures included as part of the secondary containment system are the Shield Building of each reactor unit, the Auxiliary Building, the Condensate Demineralizer Waste Evaporator (CDWE) Building and the essential raw cooling water (ERCW) pipe tunnels adjacent to the Auxiliary Building. Depending on the configuration of the plant, the Primary Containment Building(s) may also be included as a structure which is part of the secondary containment system. This condition exists when the primary containment is open to the Auxiliary Building. The emergency gas treatment system (EGTS) is provided for ventilation control and cleanup of the atmosphere inside the annulus between the Shield Building and the Primary Containment Building. The Reactor Building purge air system is also available for cleaning up the atmosphere inside the Shield Building Annulus. Refer to Section 9.4.6 for further details relating to the purge air system. The Auxiliary Building Gas Treatment System (ABGTS) provides a similar contamination control capability in the Auxiliary Building Secondary Containment Enclosure (ABSCE),which includes all of the areas listed above.
6.2.3.1 Design Bases 6.2.3.1.1 Secondary Containment Enclosures Design bases for the secondary containment structures were devised to assure that an effective barrier exists for airborne fission products that may leak from the primary containment, or the Auxiliary Building fuel handling area, during a loss-of-coolant accident (LOCA). Within the scope of these design bases are requirements that influence the size, structural integrity, and leak tightness of the secondary containment enclosure. Specifically, these include a capability to: (a) maintain an effective barrier for gases and vapors that may leak from the primary containment during all normal and abnormal events; (b) delay the release of any gases and vapors that may leak from the primary containment during accidents; (c) allow gases and vapors that may leak through the primary containment during accidents to flow into the contained air volume within the secondary containment where they are diluted, held up, and purified prior to being released to the environs; (d) bleed to the secondary containment each air-filled containment penetration enclosure which extends beyond the Shield Building and which is formed by automatically actuated isolation valves; (e) maintain an effective barrier for airborne radioactive contaminants, gases, and vapors originating in the ABSCE during normal and abnormal events.
Refer to Sections 3.8.1 and 3.8.4 for further details relating to the design of the Shield Building and the Auxiliary Building.
6.2.3.1.2 Emergency Gas Treatment System (EGTS)
The design bases for the EGTS are:
(1) To keep the air pressure within each Shield Building annulus below atmospheric pressure at all times in which the integrity of that particular containment is required.
Design Bases 6.2.3-1
WATTS BAR WBNP-112 (2) To reduce the concentration of radioactive nuclides in annulus air that is released to the environs during a LOCA in either reactor unit to levels sufficiently low to keep the site boundary and low population zone (LPZ) dose rates below the 10 CFR 100 values.
(3) To withstand the safe shutdown earthquake.
(4) To provide for initial and periodic testing of the system capability to function as designed.
6.2.3.1.3 Auxiliary Building Gas Treatment System (ABGTS)
The design bases for the ABGTS are:
(1) To establish and keep an air pressure that is below atmospheric within the portion of the buildings serving as a secondary containment enclosure during accidents.
(2) To reduce the concentration of radioactive nuclides in air releases from the secondary containment enclosures to the environs during accidents to levels sufficiently low to keep the site boundary and LPZ dose rates below the 10 CFR 100 guideline values.
(3) To minimize the spreading of airborne radioactivity within the Auxiliary Building following an accidental release in the fuel handling and waste packaging areas. ABGTS is not required to mitigate the consequences of a fuel handling accident.
(4) To withstand the safe shutdown earthquake.
(5) To provide for initial and periodic testing of the system capability to function as designed (See Chapter 14.0 for information on initial testing of systems).
6.2.3.2 System Design 6.2.3.2.1 Secondary Containment Enclosures (1) Shield Building The principal components that function collectively to form a secondary containment barrier around the steel primary containment vessel are the Shield Building itself, the Shield Building penetration seals, the isolation valves installed in the penetrations to the Shield Building, and the Shield Building penetration leakoff facilities.
Structure The Shield Building is a reinforced concrete structure that encloses the reactor's steel primary containment structure; it has a circular horizontal cross section and a shallow domed roof. The vertical center line of this building is 6.2.3-2 System Design
WATTS BAR WBNP-112 also the vertical center line of the steel primary containment vessel. The inside diameter of this building was sized to provide an annular shaped air space between the two reactor enclosures that is approximately five feet wide. The total enclosed free air space between the two enclosures is approximately 396,000 cubic feet.
Penetrations To ensure that the Shield Building provides a nearly leak tight enclosure for the primary containment structure all openings in the shield building penetrations are sealed. Typical mechanical piping or ventilation penetrations are equipped with a flexible membrane seal as shown in Figure 6.2.3-1. Mechanical penetrations are designed for a leakage rate no greater than 0.0052 cfm per square inch when secondary containment is at a minus 0.5 inch water gauge. The primary containment personnel hatch passes through the Shield Building and opens directly to the Auxiliary Building. This opening in the Shield Building wall is handled as an ordinary piping penetration and is provided with a flexible, double membrane seal as shown in Figure 3.8.2-5 (see Section 3.8.2). Personnel and equipment access doors to the secondary containment are treated as special cases and are provided with resilient seals as shown in Figures 3.8.4-21 through 3.8.4-23. (See Section 3.8.4 for descriptions of the personnel access doors and the equipment access doors.) The allowable leakage for each personnel access door is 0.5 cfm when secondary containment is at minus 1 inch water gauge, and 10 cfm for the equipment access hatch when secondary containment is at minus 0.75 inch water gauge.
Air filled lines which must be isolated by automatic valve actuation and which penetrate both the primary containment and the shield building are considered more likely to pass airborne radioactivities than other lines.
Therefore these lines are provided with a third isolation valve outside the secondary containment for additional leak protection. This single, third valve receives both Train A and B actuation signals. Buffering prevents an electrical failure in one train from affecting the performance of the other train.
To enhance the effectiveness of the third isolation valve as a barrier to leakage, the enclosed volume between the second and third isolation valves is opened to the annulus at all times. Opening this enclosed space to the annulus is accomplished with leakoff facilities as shown in Figure 6.2.3-2.
This allows the negative pressure in the annulus to include this small volume, and leakage from the primary containment outward or leakage from outside the Shield Building inward to be drawn into the annulus for processing. The lines provided with this feature are those for the primary containment purge supply and exhaust. The 8-inch lower compartment pressure relief line is excluded from this consideration since it terminates in the annulus through a filter train and does not go outside the Shield Building.
Electrical penetrations are of either a cable tray/cable slot type or a conduit type. Typical seals for these penetrations are shown in Figure 6.2.3-3. For System Design 6.2.3-3
WATTS BAR WBNP-112 cable tray/cable slot penetrations, silicone room temperature vulcanizing (RTV) foam is used as the sealant around cables within the wall opening over a portion of the length of the cable slot penetration. In conduit penetrations, the interstitial spaces between cables and conduit or condulet walls are filled with RTV silicone rubber as the sealant over a portion of the length of the penetration. Electrical penetrations are designed for a leakage rate not greater than 0.014 cfm per square inch when secondary containment is at a minus 0.5 inch water gauge.
The total expected infiltration rate across all leakage paths into the annulus is 250 cfm at the post accident annulus control setpoint for a postulated single failure of one EGTS train (see Section 6.2.3.3.2 for a discussion of infiltration rate associated with a postulated single failure of one pressure control train).
During normal operation the annulus pressure is maintained at or more negative than 5.0 inches water gauge with respect to the outside atmosphere. Periodic tests demonstrate that inleakage is less than this value.
The fraction of primary containment leakage which may bypass the Shield Building and go directly to the Auxiliary Building is specified to be no greater than 25% of the total primary containment out-leakage. Permitting this leakage fraction results in acceptable site boundary and LPZ doses for the LOCA condition as described in Chapter 15. There are no significant paths by which primary containment leakage may bypass both the Shield Building and the Auxiliary Building and result in exceeding the offsite dose limits.
Information concerning isolation features utilized in support of the secondary containment is presented in Section 6.2.4. Potential leakage paths by which primary containment leakage could bypass the secondary containment, and measures utilized to prevent such leakage are also discussed in Section 6.2.4.
(2) Auxiliary Building Structure The Auxiliary Building provides an isolation barrier during certain postulated accidents involving airborne radioactive contamination. Certain of the buildings interior and exterior walls, floor slabs, and a part of its roof form the isolation barrier as shown in Figures 6.2.3-4 through 6.2.3-10. The enclosed volume of this isolation barrier, the ABSCE, is approximately 6.9 x 106 cubic feet. The ABSCE is discussed in more detail in Section 3 below. Additional data on the Auxiliary Building is provided in Section 3.8.4 and Table 6.2.3-1.
(3) Auxiliary Building Secondary Containment Enclosure (ABSCE)
The Auxiliary Building secondary containment enclosure (ABSCE) is that portion of the Auxiliary Building and CDWE Building (and for certain configurations, the annulus and primary containment, as discussed below) 6.2.3-4 System Design
WATTS BAR WBNP-112 which serves to maintain an effective barrier for airborne radioactive contaminants released in the auxiliary building during abnormal events.
Mechanical and electrical penetrations of this enclosure are provided with seals to minimize infiltration. Piping penetrations are either analyzed to pressure boundary retention requirements, or the effects of their failure are demonstrated not to impair the ability of the ABGTS system to maintain the ABSCE under the required negative pressure of 0.25 inches w.g., or they are isolated by physical means (e.g., locked-closed valves, etc.) Airlock-type doors are provided at portals where needed by the frequency of use. The negative pressure is maintained within the ABSCE to ensure that no contaminated air is released to the environs following an abnormal event without first being processed by the ABGTS. The ABSCE is shown in Figures 6.2.3-4 though 6.2.3-9.
Entrances and exits to those portions of the Auxiliary Building within the primary containment barrier for both equipment and personnel are through air locks. The air lock locations are shown in Figures 1.2-3 and 1.2-5. The doors in each air lock are electrically interlocked such that only one side of the air lock can be opened at a time. A control room alarm is provided should both sides of an air lock ever be opened simultaneously. As a safety precaution, an interlock defeat switch is mounted on the containment side of each air lock to allow emergency egress should either side of the air lock be blocked open in an accident.
A special case is the interlock system for the large exterior door to the railway loading area. When the large railroad access door is open, ABSCE airlock doors, such as the doors to the Post Accident Sampling Facility (PASF) and nitrogen storage area nor the access hatches above can be opened, and when either of these two doors and either of the access hatches above are open, the large railway access door cannot be opened. Administrative controls are provided to control doors and hatches during normal operation.
The railway access doors and hatches are described in Section 3.8.4.
The total permissible leakage rate for the ABSCE at a pressure of -0.25 inches water gauge with respect to the outside is 9900 cfm maximum. This represents 165.5% of the ABSCE free volume per day. Periodic tests demonstrate that inleakage is less than the design value. Any improvement in the inleakage recorded during subsequent tests shall be used to establish the allowable margin for breaching permits.
During periods when the primary containment and/or annulus of both units are open to the Auxiliary Building, the ABSCE also includes these areas. A Containment Isolation Phase A (SI Signal) from the operating unit or high temperature in the Unit 1 or Unit 2 Auxiliary Building air intake, or manual ABI will cause a CVI signal in the refueling unit. These actions will ensure proper operation of the ABSCE. Both doors of the containment vessel personnel airlocks may be open at the same time during refueling activities while the purge air ventilation system is operating. During fuel handling operations in System Design 6.2.3-5
WATTS BAR WBNP-112 this configuration, a high radiation signal from spent fuel pool radiation monitors will result in a Containment Ventilation Isolation (CVI) in addition to an Auxiliary Building isolation and ABGTS start. Similarly, a CVI signal, including a CVI signal generated by a high radiation signal from the containment purge air exhaust radition monitors, will initiate an Auxiliary Building isolation and start of ABGTS. These are not required functions for the ABGTS and the Reactor Building Purge Systems filters or for Purge System isolation as no credit for these features is in mitigating a fuel handling accident. In the case where containment of both units is open to the Auxiliary Building spaces, a CVI in one unit will initiate a CVI in the other unit in order to maintain those spaces open to the ABSCE.
Doors and penetrations of the ABSCE perimeter are provided with seals to reduce infiltration. Doors and hatches entering the area are either locked or under administrative control.
Automatic redundant isolation dampers are provided in ducts which pass from areas inside the ABSCE to areas outside of the enclosure. These permit isolation of the ABSCE and allow the ABGTS to maintain a negative pressure in the area following an abnormal event.
The ABGTS maintains a negative pressure with respect to the outside in the ABSCE during emergency operation and processes the Auxiliary Building exhaust. Either train of the ABGTS may be used to maintain the negative pressure and treat air exhausted from the ABSCE.
The annulus vacuum control subsystem continues to operate whenever the ABSCE is isolated, except for a Phase A containment isolation signal. A Phase A containment isolation signal which is generated by a LOCA starts the air cleanup subsystem of the emergency gas treatment system.
Calculations have shown that this condition does not result in exceeding the limits given in 10 CFR 100. For additional description of the annulus vacuum control subsystem of the EGTS, see Section 6.2.3.2.2.
Proper actuation of the isolation dampers associated with the ABSCE and operation of the ABGTS is confirmed periodically.
6.2.3.2.2 Emergency Gas Treatment System (EGTS)
The EGTS is shown schematically in Figure 6.2.3-11. The logic and control diagrams for this system are shown in Figures 6.2.3-12 to 6.2.3-15A. This system has two subsystems: the annulus vacuum control subsystem and the air cleanup subsystem.
The portions of the EGTS necessary to ensure that the system performs its functions during post-accident operation are classified Seismic Category I. Portions of the system which are not necessary for post-accident operation are seismically qualified to the extent that the system does not adversely affect any safety-related system(s)/component(s) as a result of its failure due to the seismic event; that is qualified Seismic Category I(L).
6.2.3-6 System Design
WATTS BAR WBNP-112 Annulus Vacuum Control Subsystem The annulus vacuum control subsystem is a fan and duct network used to establish and keep a negative pressure level within the annular space between the primary and secondary containment structures. It is utilized during normal operations in which containment integrity is required. In emergencies in which containment isolation is required, this subsystem is isolated and shut down. This subsystem performs no safety-related function. Because of this, the annulus vacuum control subsystem is not classified as an engineered safety feature.
This subsystem has two independently controlled branches. Each branch serves one reactor unit. These branches draw air from their assigned annuli and release it into the Auxiliary Building Fuel Handling Area exhaust duct system. The air inlet for each branch is centrally located in its respective secondary containment volume above the steel containment dome.
Air pressure control in each secondary containment annulus is achieved with one of the two, 100% capacity redundant fans, a differential pressure sensor, motor operated damper and control circuitry installation incorporated into each branch. This equipment provides a capability to vary the volumetric flow rate drawn from the annulus to keep the pressure at a predetermined negative pressure level. This control function is accomplished with a modulating damper under control of a differential pressure sensor that adjusts the amount of outside air introduced upstream of a constant capacity fan in the proper manner to keep the annulus pressure within a designated narrow range. One of the two redundant units starts automatically in the event the operating control unit fails to function in the proper manner.
The fans and flow control dampers serving the reactor secondary containment annulus are installed in the EGTS room at Elevation 757.0' adjacent to the Unit 2 Shield Building.
The nominal negative pressure for the annulus vacuum control equipment installation is 5 inches of water gauge. The controller setpoint is established such that the annulus pressure is maintained at, or more negative than, 5 inches water gauge. This negative pressure level chosen for normal operation ensures that the annulus pressure will not reach positive values during the annulus pressure surge produced by a LOCA in the primary containment. Two 100% capacity fans are utilized to maintain this negative pressure. One fan is normally on standby.
Annulus vacuum control subsystem aids in containment pressure relief by exhausting the containment vent air after it goes through the containment vent air clean up units and is discharged into the annulus then into the Auxiliary Building exhaust stack (See Section 9.4.6).
Air Cleanup Subsystem The air cleanup subsystem is a redundant, shared airflow network having the capability to perform two functions for the affected reactor secondary containment during a LOCA. One of these is to keep the secondary containment annulus air volume below System Design 6.2.3-7
WATTS BAR WBNP-112 atmospheric pressure. The second function is to remove airborne particulates and vapors that may contain radioactive nuclides from air drawn from the annulus. Each of these is accomplished by this subsystem without disturbing operation of the unaffected reactor unit.
Both of these functions are performed by processing and controlling a stream of air taken from the reactor unit secondary containment annulus. The air cleanup operation is conducted by drawing the air stream through a series of filters and adsorbers.
Annulus air pressure control is accomplished by adjusting the fraction of the airstream that is returned to the annulus air space.
The negative pressure control setpoint chosen for post-accident operation is low enough that leakage across the boundary is into the annulus from both the primary containment and areas adjacent to the Shield Building. The pressure differentials produced by wind effects are also overcome by appropriate selection of the annulus negative pressure level.
The rated capacity of each redundant air cleanup unit in the subsystem is 4000 cfm.
This subsystem of the EGTS is classified as an engineered safety feature.
The air flow network for the air cleanup subsystem was designed to provide the redundant services needed for either reactor secondary containment annulus. The suction-side ductwork in this network which is used to bring annulus air to the EGTS room on Elevation 757.0' in the Auxiliary Building is also used by the annulus vacuum control subsystem. The intake is centrally located within the Shield Building above the steel containment dome. Within the EGTS room the network branches out in a manner to supply two air cleanup unit installations that can be aligned with flow control dampers to serve either annulus air volume. After the air is processed through the air cleanup subsystem, it is routed to the redundant damper controlled flow dividers in the annulus. Inside each annulus, the air flow network contains two air flow paths: one leading to the Shield Building vent and the other to a manifold that distributes and releases the air uniformly around the bottom of the annulus.
The vertical separation between the intake above the dome and the exhaust ports in the manifold is approximately 168 feet. Butterfly valves, rather than dampers, are installed in the ducts just above the flow distribution manifold to minimize the outside air inleakage from the reactor unit vents into the annulus.
Another feature incorporated into the air cleanup subsystem air flow network is the capability to cool the filters and adsorbers in an inactive air cleanup unit that is loaded with radioactive material. This is accomplished with two cross-over flow ducts that can draw air at a minumum of 200 cfm from the active air cleanup unit through the inactive air cleanup unit. (Such an air flow is sufficient to keep the temperature rise through a fully loaded inactive air cleanup unit to less than 75°F.) Two butterfly valves in series are installed in each cross-over air flow path to assure sufficient isolation to perform accurate removal efficiency tests on the HEPA filter and carbon absorber banks. This feature is provided in the event excessive adsorber bed temperature occurs following the failure of an operating EGTS train. Adsorber bed temperature is indicated and 6.2.3-8 System Design
WATTS BAR WBNP-112 supplied to the plant process computer. Status indication of each EGTS train is also provided. Upon failure of an operating EGTS train, adsorber bed temperature is monitored to detect subsequent temperature rise. After a Phase A containment isolation signal has initiated EGTS operation, the control room operator will shut one of the two EGTS trains down and align the appropriate butterfly valves for automatic operation. In addition, the associated suction valve is remotely opened from the main control room to establish a flow path from the annulus through the air cleanup unit.
The two air cleanup units in the air cleanup subsystem have stainless steel housings containing air treatment equipment, sampling ports, heaters, drains, test fittings, and access facilities for maintenance. See Section 6.5.1.2.1 for a description of the air cleanup units and information related to their design.
A centrifugal fan is provided outside each air cleanup unit housing. These fans were designed to function in process air flow streams at temperatures up to 200°F. See Table 6.2.3-1 for additional information on these fans.
Two air flow control modules are also included in the air cleanup subsystem. Each consists of a differential pressure sensor and transmitter, control circuitry, a damper actuator, and two modulating dampers. The single damper actuator adjusts the dampers simultaneously in opposite directions, i.e., one is closed as the other is opened.
A pressure control system with a station located in the main control room modulates pressure control dampers in the annulus to maintain the differential pressure setpoint.
Two sets of independent pressure control dampers installed in the secondary containment annulus provide the capability to adjust the amount of air recirculated to the reactor unit annulus or discharged to the shield building exhaust vent. Annulus pressures that are more positive than the pressure controller setpoint produce a signal causing the damper actuator to begin closing the damper controlling the air flow to the annulus and to start opening the damper controlling the air flow to the Shield Building exhaust vent. Annulus pressures that are more negative than the pressure controller setpoint initiate the opposite kind of damper motions.
Four isolation valves (two valves per train) installed in the secondary containment annulus provide isolation of the pressure control dampers. Each train has a handswitch in the control room positioned so that both trains of isolation valves are in A-AUTO . A containment isolation Phase A signal causes the valves to open. The open isolation valves provide a flow path for both trains of pressure control dampers which modulate to control annulus pressure. For further details, see Figures 6.2.3-14 and 6.2.3-15.
Operation of the air cleanup subsystem during accidents is initiated by the Phase A containment isolation signal. Both the A and the B trains start and damper alignment initiated by this signal. A capability is also provided to start each fan with a hand switch in the main control room. Damper alignment is also initiated by the same signal.
Another adjustment of hand switches in the main control room changes the operating mode to the single train operation with the redundant fan in a standby status.
System Design 6.2.3-9
WATTS BAR WBNP-112 Employment of this operating mode is required after 1 hour1.157407e-5 days <br />2.777778e-4 hours <br />1.653439e-6 weeks <br />3.805e-7 months <br /> and before 2 hours2.314815e-5 days <br />5.555556e-4 hours <br />3.306878e-6 weeks <br />7.61e-7 months <br /> of operation. The control room operator can select either train to remain in operation.
6.2.3.2.3 Auxiliary Building Gas Treatment System (ABGTS)
The ABGTS is a fully redundant air cleanup network provided to reduce radioactive nuclide releases from the secondary containment enclosure during accidents. It does this by drawing air from the fuel handling and waste packaging areas through ducting normally used for ventilation purposes to air cleanup equipment, and then directing this air to the reactor unit vent. In doing so, this system draws air from all parts of the ABSCE to establish a negative pressure region in which virtually no unprocessed air passes from this secondary containment enclosure to the atmosphere.
During periods when the primary containment and/or annulus of both units are open to the Auxiliary Building, the ABSCE also includes these areas. The ABGTS has been designed to establish a negative pressure in these additional areas for this configuration. During fuel handling operations in this configuration, a high radiation signal from the spent fuel pool radiation monitors will result in a Containment Ventilation Isolation (CVI) in addition to an Auxiliary Building isolation and ABGTS start. Similarly, a CVI signal, including a CVI signal generated by a high radiation signal from the containment purge air exhaust radiation monitors, will initiate an Auxiliary Building isolation and start of ABGTS. Likewise, a Containment Isolation Phase A (SI Signal) from the operating unit or high temperature in the Unit 1 or Unit 2 Auxiliary Building air intake, or manual ABI will cause a CVI signal in the refueling unit. These actions will ensure proper operation of the ABSCE. However, as an added precaution to protect the ABGTS operational boundary, operational action is needed to ensure the closure of the containment purge exhaust isolation valves (system valves not containment isolation valves) which are controlled by hand switches. In the case where containment of both units is open to the Auxiliary Building spaces, a CVI in one unit will initiate a CVI in the other unit in order to maintain those spaces open to the ABSCE.
Although the ABGTS is available to minimize the consequences of a fuel handling accident, it is not required to function in order to meet control room and offsite dose limits based on the use of the Regulatory Guide 1.183, Revision 0 (Alternate Source Term) methodology.
The portions of the ABGTS that are required to ensure that the system functions properly are classified Seismic Category I. Certain portions of the system, which are not required for post-accident operation of the ABGTS, are seismically qualified to the extent that system operation is not adversely affected should they fail due to the seismic event (i.e., classified according to Seismic Category I(L)).
The rated capacity of each redundant ABGTS air cleanup unit (ACU) is 9000 cfm.
These ACUs were designed in accordance with engineered safety feature standards.
The unique portions of the ABGTS are shown schematically in Figures 6.2.3-16 and 9.4-8. Logic and control diagrams for the ABGTS are shown in Figures 9.4-10 and 9.4-17. The airflow network for this system consists of the exhaust ductwork, which normally serves the fuel handling and waste packaging areas connected to the 6.2.3-10 System Design
WATTS BAR WBNP-112 suction-side of the Train A ACU, and a cross-over duct which connects the ductwork with the suction-side of the Train B ACU. The discharges from the Train A and Train B ABGTS exhaust fans separately go to the Unit 1 and Unit 2 Shield Building exhaust vents, respectively.
The air flow ductwork that is not unique to this system consists of some of the normal ventilation ducting installed in the ABSCE. When the ABSCE is isolated, this duct network provides a flow path for the ABGTS to draw down and maintains a negative pressure in ABSCE. In some instances, air is drawn in the opposite direction to the normal air flow pattern during operation of the ABGTS. Each ACU includes air treatment components, instrumentation, test fittings, and other equipment required for proper operations and testing of the system. Refer to Section 6.5.1.2.2 for a description of the ABGTS air cleanup units and information related to their design.
Information on these fans is given in Table 6.2.3-1.
The air flow control modules utilized in the ABGTS contain a differential pressure sensor and transmitter, control circuitry, and a modulating damper. These air flow control modules provide the capability for keeping the pressure within the ABSCE at a minimum of 1/4 inch water gauge below atmospheric with the differential pressure transmitter and differential pressure controller circuit adjusting the amount of outside air admitted into the duct network by the vacuum relief line. Such action brings in sufficient outside air to keep the fan flow rate at its rated flow at all times.
The negative pressure level chosen for post-accident operation is sufficiently low to ensure that airborne contamination present in the Auxiliary Building is not released to the environs without being processed by an air cleanup assembly. External pressure gradients produced by outside temperature and wind loadings on the building do not adversely affect the ability of the ABGTS to maintain the negative pressure in the ABSCE.
The controls for the ABGTS are designed to provide two basic control modes. One control mode has either one of the air cleanup units in operation and the other in a state in which the redundant unit can automatically come into operation in the event the operating unit fails. Less negative than adequate pressure in the ABSCE is utilized in this control mode to make this failure determination. This operational redundancy is achieved with spatially separated power and control circuitry having different independent power sources to prevent a loss of function from any single system component failure. The term "Train A" is used to identify one complete set of full capacity equipment and the term "Train B" is used to identify the other set of full capacity equipment. Power for both equipment trains is supplied by the emergency power system.
Operation of the ABGTS begins automatically upon initiation of an high radiation signal from the spent fuel pool accident radiation monitors or an ABI signal which is generated from one of the following signals:
(1) Phase A containment isolation signal, or System Design 6.2.3-11
WATTS BAR WBNP-112 (2) High temperature signal from the Unit 1 and Unit 2 Auxiliary Building air intakes.
Additionally, during refueling operations when containment and/or the annulus is open to the Auxiliary Building ABSCE spaces, a containment vent isolation signal from either the operating unit or refueling unit will automatically start the ABGTS.
A capability is also provided to start each train with a hand switch (one hand switch per train) in the main control room. Another adjustment capability provided in the hand switches in the main control room changes the operating mode to the single train operation with the redundant train in a standby status. Employment of this operating mode is expected after the first 30 minutes of operation. In this instance, the main control room operator has the capability to select either train to remain in operation.
The standby unit selected automatically starts in the event the operating unit does not adequately maintain negative pressure in the ABSCE.
6.2.3.3 Design Evaluation 6.2.3.3.1 Secondary Containment Enclosures The secondary containment enclosures are designed to provide a positive barrier to all potential primary containment leakage pathways during a LOCA and to radioactive contaminants released in accidental spills and fuel handling accidents that may occur in the ABSCE. In a LOCA, the Shield Building containment enclosure provides the barrier to all airborne primary containment leakage, and the ABSCE provides a barrier to through-the-line leakage which can potentially become airborne. The ABSCE also maintains an effective barrier for airborne radioactive contaminants originating inside the ABSCE during normal and abnormal events. The original design credited the secondary containment enclosures to mitigate the consequences of a FHA. Although these enclosures are available to minimize the consequences of a FHA, based on the use of the Regulatory Guide 1.183, Revision 0 (Alternate Source Term) methodology for a FHA, the structures are no longer required for mitigation of a postulated FHA.
(1) Shield Building Structure The Shield Building provides the physical barrier for airborne primary containment leakage during a LOCA. Because the Shield Building completely encloses the free standing primary containment, most of the airborne leakage from primary containment passes into the annular region provided by this arrangement.
The building construction employs monolithic pours of concrete. This approach for structures of this type produces a very low leakage barrier. The low leakage characteristics of this barrier help to reduce the rate at which purified annulus air must be released to maintain the enclosed volume at a negative pressure. This factor contributes significantly to keeping the site boundary and the low population zone (LPZ) dosage levels within 10 CFR 100 guidelines.
6.2.3-12 Design Evaluation
WATTS BAR WBNP-112 The design of the EGTS system and the size of the annular region between the primary containment and the shield building assures a residence time for all leakage into the annulus.
Penetrations The Shield Building wall is provided with many penetrations to accommodate mechanical equipment piping, cable trays, and electrical conduit which leave and enter the Shield Building. Due to the low leakage characteristics of the building, leakage through the Shield Building wall is restricted almost entirely to openings in these penetrations. The design assures that penetration leakage does not exceed predetermined quantities. Such a capability ensures that the inleakage is sufficiently low to keep the dose contributions at the site boundary and to the LPZ within 10 CFR 100 guidelines.
Openings in mechanical piping penetrations are sealed principally as shown in Figure 6.2.3-1. The seals are a flexible membrane type of single gaskets which incorporate fire resistant materials and are designed to withstand the combinations of Shield Building and piping movements in the SSE and retain their functional integrity. In addition, seals at or below the probable maximum flood elevation are designed to be water tight for flood static head and surge forces. All seals, where possible, are installed outside the Shield Building such that whether during normal operation, accidents, or flood, the differential pressures will tend to enhance the tightness of the seal. The penetration seal materials have been selected to be compatible with the maximum design integrated dose for the Shield Building during a LOCA.
Cables routed in cable trays pass through the Shield Building wall through rectangular cable slot penetrations as shown in Figure 6.2.3-3. The sealant material installed around cables over a portion of the length of the cable slot is silicone RTV (room temperature vulcanizing) foam and is RTV silicone rubber installed around cables within conduits. The seals are typically shown in Figure 6.2.3-3 and are designed to withstand the SSE and retain their integrity. Electrical penetration seals are allowed twice the leakage of mechanical seals to provide sufficient margin in meeting the total allowable Shield Building leakage requirements.
The personnel and equipment access doors to the Shield Building are designed with heat resistant, resilient seals which reduce their leakage to the allowable values as stated in Section 6.2.3.2. These doors are designed to retain their structural integrity and leak tightness during a SSE as described in Sections 3.8.1 and 3.8.2.
To allow personnel access to the annulus during operation, the annulus personnel access doors form an airlock. The doors are electrically interlocked such that only one of the pair may be opened at a time, but an electric interlock defeat switch is provided inside the annulus to provide for emergency egress from the annulus Design Evaluation 6.2.3-13
WATTS BAR WBNP-112 should the door on the Auxiliary Building side of the lock be blocked open during an accident. Therefore, a continuous secondary containment barrier is provided while allowing personnel movement.
The fuel transfer tubes penetrate the primary and secondary containment on their way to the Auxiliary Building. Each transfer tube has a blind flange on the inboard side of primary containment, equipped with double seals and a pressure test connection between the seals. The valve in the Auxiliary Building end of the transfer tube serves as the secondary containment isolation valve. The inner space between the primary containment flange and the isolation valve is bled to the annulus so that any leakage into the tube from primary containment or the Auxiliary Building flows into the annulus. The bleed line is routed above the maximum refueling pool water level to preclude accidental spills of refueling water.
(2) Auxiliary Building Structure The entire Auxiliary Building including walls, roof, and interior partitions is constructed by consecutive monolithic pours of concrete. This method of assembly produces a structure with very low leakage characteristics. The portions of the building chosen to constitute the isolation barrier were selected such that sources of potential contamination are completely enclosed. Therefore, the structure utilized to form the Auxiliary Building containment envelope functions effectively as a barrier to the environs. This same structure also helps to reduce inleakage into the Auxiliary Building containment envelope during accidents to levels easily accommodated by the ABGTS.
Penetrations Seals for mechanical penetrations are a flexible membrane type or single gaskets. The seals are designed to withstand Auxiliary Building and piping movements in the SSE and retain their structural integrity. The materials chosen for the seals are fire resistant. The seals, where possible, are designed such that whether during normal operation or accidents, the differential pressures tend to enhance the tightness of the seal. Sealing methods for electrical penetrations are similar to those for the Shield Building electrical penetrations.
Each normal ventilation duct penetrating the ABSCE is equipped with two isolation dampers in series. The dampers have resilient blade end and blade edge seals which are designed to retain their functional characteristics. The motor operators for these dampers have been sized to tightly close the damper blades against their resilient seals. The damper and motor operator assemblies are designed to operate during and after the SSE.
6.2.3-14 Design Evaluation
WATTS BAR WBNP-112 Piping penetrations are analyzed to pressure boundary retention requirements.
The effects of piping penetration failures are demonstrated to not impair the ability of the ABGTS system to maintain the ABSCE pressure boundary (under the required negative pressure of 0.25 inches w.g.), or the penetrations are isolated by physical means (e.g., locked-closed valves).
6.2.3.3.2 Emergency Gas Treatment System (EGTS)
The EGTS has the capabilities needed to preserve safety in accidents as severe as the design basis LOCA. To verify that the proper features are provided, functional analyses were conducted which consist of failure modes and effects analysis of the system, reviews of Regulatory Guide 1.52 sections to assure licensing requirement conformance, and performance analyses to verify that the system has the desired accident mitigation capabilities. A detailed failure modes and effects analysis is presented in Table 6.2.3-2. The system is shown schematically in Figure 6.2.3-11.
The functional analyses conducted on the EGTS have shown that:
(1) Adequate isolation of the annulus vacuum control subsystem during accidents is provided. The two low leakage valves in series upstream of the annulus vacuum control subsystem fans used to isolate the two subsystems--one operated by each subsystem train--give assurance that the annulus vacuum control subsystem will be isolated during accidents. These valves fail closed.
(2) The air flow control dampers in the air cleanup subsystem align to service the affected reactor units. The network was designed to have the air flow control dampers shown in Figures 6.2.3-18 and 6.2.3-19 needed to service a particular reactor unit responsive to only the containment isolation signal from that particular reactor unit.
(3) The system intake and recirculation air outlets, shown on Figures 6.2.3-18 and 6.2.3-19, within the Shield Building annulus are positioned to promote mixing and dilution of primary containment leakage. Positioning the recirculation air manifold and the air outlets almost completely around the base of the annulus below the level of the containment penetrations assures a clean air flow past most of the penetrations. This air, warmed by the relative humidity heater, flows upward past these likely sources of leakage. In doing so, the flow impediments (i.e., penetrations, and structures within the annulus) tend to redirect this air flow to induce mixing and dilution.
Substantial amounts of mixing and dilution are likely in the vertical rise of over 168 feet to the system air intake above the steel containment dome.
(4) System startup reliability is very high. The practice of automatically starting up both full capacity trains in the system simultaneously gives greater assurance that one train of equipment functions promptly upon receipt of an accident signal.
Design Evaluation 6.2.3-15
WATTS BAR WBNP-112 (5) The use of a single actuator in each equipment train to adjust dampers controlling the air flow recirculated and vented improves train reliability and minimizes the possibility of annulus pressure instability. Simultaneous adjustment that closes one damper and opens the other eliminates the hunting problems that could arise from nonsimultaneous operation of separately actuated dampers.
(6) The Train A and Train B air cleanup units are adequately protected from each other to eliminate the possibility of a single failure destroying the capability to process annulus air during emergencies. The 13.5 feet high and 27 inch thick concrete wall built between the two units protects each from missiles originating in the other unit.
The EGTS, designed prior to issuance of Regulatory Guide 1.52, is in general agreement with requirements in the guide. Details on this compliance with Regulatory Guide 1.52 are given in Table 6.5-1.
The performance analyses conducted to verify that the EGTS has the required accident mitigation capabilities were conducted in three basic parts. One of these was concerned with the capability for keeping the Shield Building annulus below atmospheric pressure at all times during a LOCA. The second part was an analysis of the cooling capabilities provided to keep temperatures within filters and adsorbers fully loaded with radioactive nuclides at safe levels. The third part was concerned with the site boundary and LPZ dosage contribution from radioactive nuclides present in annulus air releases during the design basis LOCA. These three analyses are discussed under the respective headings below.
Annulus Negative Pressure Control Capability The capability of the EGTS to keep the Shield Building annulus below atmospheric pressure during a design basis LOCA was established with a time iteration analysis performed by a computer. Energy and mass balances were accomplished successively in accordance with mass and volume changes calculated to take place during each time increment. Such a methodology allowed sufficient freedom to account for:
(1) Steel containment vessel growth from internal pressure, (2) Steel containment vessel growth from thermal expansion, (3) Outside air inleakage into the Shield Building annulus, and (4) Heat transfer from the steel containment structure to the annulus air mass.
To assure that this analysis was valid and conservative:
(1) Heat transfer from the primary containment atmosphere to the primary containment vessel was assumed to be convective. An air-steam mixture convective heat transfer coefficient was chosen to maximize heat transfer to 6.2.3-16 Design Evaluation
WATTS BAR WBNP-112 the secondary containment atmosphere. The constant value of 400 Btu/hr-ft2-°F given in Table 6.2.3-1 compares conservatively to the integrated transient heat transfer coefficients recommended in Branch Technical Position CSB 6-1. Heat transfer from the primary containment vessel to the annulus atmosphere and from the atmosphere to the secondary containment wall was assumed to be convective. Heat transfer from the primary containment vessel to the secondary containment wall was assumed to be by radiation. Forms of the transient convective heat transfer coefficients and values for the constant radiative heat transfer coefficients are given in Table 6.2.3-1. Consideration was given to the heat capacity of both the primary and secondary containment structures. The thermal conductivity and capacitance for these walls, as given in Table 6.2.3-1, agree closely with those obtained from Branch Technical Position CSB 6-1.
(2) The thermal growth of the steel vessel was based on linear expansion which was applied to the transient containment vessel temperature increases above the initial steady-state values to obtain the transient radial expansion (see Table 6.2.3-1 for total containment expansion). Temperature gradients were calculated for three regions: upper compartment, ice condenser, and lower compartment. The radial expansions in each of these three regions were converted to volume changes which were summed to yield a total annulus volume change due to primary containment vessel thermal expansion.
(3) Table 6.2.3-1 presents the characteristics of the internal pressure effects on the containment vessel. This model uses linear elastic thin shell theory to determine the expansion. The cylindrical portion of the vessel is assumed to act as a cylindrical shell with capped ends. The hemispherical dome expands uniformly as a simple sphere and includes the axial expansion of the cylinder.
External vertical and circumferential stiffeners are assumed not to be present so that conservative results are obtained. This pressure-induced growth was assumed to occur instantaneously at the start of the LOCA.
(4) Air leakage into the Shield Building annulus was assumed to be 250 cfm at the post accident annulus control setpoint for a postulated single failure of one EGTS train. A more conservative air inleakage value of 832 cfm was assumed for an alternate single failure scenario which results in one pressure control train in full exhaust to the shield building exhaust stack while the other train remains functional. This higher inleakage value is based upon the higher negative pressure that will exist within the annulus during this scenario.
(5) The air temperature in the annulus was assumed to be a thermally mixed average.
Design Evaluation 6.2.3-17
WATTS BAR WBNP-112 (6) Only one train of the EGTS was assumed to operate during the first single failure scenario, allowing for a possible single failure in the other. An alternate single failure scenario was analyzed which postulates one pressure control train failing which results in full exhaust to the shield building exhaust stack while the other train remains functional.
The initial steady state conditions used in this analysis were as follows (refer also to Table 6.2.3-1):
Relative Pressure Temperature Humidity Containment upper compartment atm. 110°F 0%
Ice condenser compartment atm. 15°F 0%
Containment lower compartment atm. 120°F 0%
Shield Building annulus -5 in. w.g. 50°F 0%
Outside atm. 0° 0%
These initial values were chosen to maximize the secondary containment pressure after the LOCA. The initial pressure of minus 5.0 inches of water gauge with respect to the outside is the pressure maintained by the annulus vacuum control subsystem during normal operation. The initial temperature of 50°F is the estimated minimum temperature which was assumed for maximum annulus air density. Similarly, the initial relative humidity of 0% was assumed for maximum annulus air density for conservatism.
The results obtained from this analysis for the first single failure scenario are shown in Figure 6.2.3-17. This annulus pressure and EGTS exhaust rate vs. time curve indicates that, after the initial containment pressure induced step increase, the pressure rises to a peak value of approximately minus 1.06 inch of water in about 79 seconds after the LOCA begins. The annulus pressure is then restored and maintained at or below the EGTS setpoint value as shown in Figure 6.2.3-17.
The results obtained from the analysis for the alternate single failure scenario are shown in Figure 6.2.3-17A. This annulus pressure and EGTS exhaust rate vs. time curve indicates that, after the initial containment pressure induced step increase, the pressure rises to a peak value of approximately minus 1.52 inch of water in about 50 seconds after the LOCA begins. The annulus pressure is then restored and maintained at or below the EGTS setpoint value as shown in Figure 6.2.3-17A.
The expansion of approximately 1,234 ft3 due to internal temperature summed with the expansion of 766 ft3 from internal pressure yields a total primary containment vessel expansion of approximately 2,000 ft3. Such results indicate that:
6.2.3-18 Design Evaluation
WATTS BAR WBNP-112 (1) The negative pressure level of 5 inches of water below atmospheric in the Shield Building annulus maintained by the annulus vacuum control subsystem before an accident minimizes the amount of unfiltered radioactive nuclides potentially released to the environment before the air cleanup subsystem becomes operational.
(2) The rated flow rate of 4000 +/-10% cfm for each train of the air cleanup subsystem is adequate to keep the annulus pressure below the negative pressure setpoint throughout the remaining period of the LOCA.
Inactive Air Cleanup Unit Cooling Capabilities The second performance analysis conducted to show that the EGTS can cope with circumstances that may occur in a LOCA was concerned with temperature control capabilities provided for air filters and adsorbers loaded with radioactive material. The analysis conducted assumed accident releases in accordance with Regulatory Guide 1.89 (100% noble gas activity, 50% iodines, and 1% particulates) and containment leakages of 0.25% per/day for the first day and 0.125% per/day from one to 100 days in accordance with Regulatory Guide 1.4. An additional assumption made was that the gamma and beta energy releases were transformed into heat within the filters and absorbers.
This occurs a few days after the LOCA takes place. The design objective is to assure that the air cleanup unit component temperatures do not exceed 200°F; it was found that a cooling air flow rate of 112 cfm is required. Such results indicate that the cooling air flow rate of 200 cfm provided for this purpose should keep the temperature within the carbon adsorber bank well below the 620°F carbon ignition temperature.
Site Boundary and LPZ Dosage Contributions The last performance analysis conducted to show that the EGTS has the capability to perform in the required manner to preserve safety during a LOCA was concerned with the site boundary and LPZ dosage contributions arising from annulus air releases to the environs. This analysis is described and evaluated in Chapter 15.
6.2.3.3.3 Auxiliary Building Gas Treatment System (ABGTS)
The ABGTS has the capabilities needed to preserve safety in accidents as severe as a LOCA. This was determined by conducting functional analyses of the system to verify that the system has the proper features for accident mitigation which consist of a failure modes and effects analysis, a review of Regulatory Guide 1.52 sections to assure licensing requirement conformance, and a performance analysis to verify that the system has the desired accident mitigation capabilities. A detailed failure modes and effects analysis is presented in Table 6.2.3-3.
The functional analyses conducted on the ABGTS have shown that:
(1) The air intakes for the system are properly located to minimize accident effects. The use of the air intakes provided in the fuel handling and waste disposal areas minimizes the spread of airborne contamination that may be Design Evaluation 6.2.3-19
WATTS BAR WBNP-112 accidentally released at these positions in which the probability of an accidental release, e.g., a fuel handling accident, is more likely. This localization effect is provided without reducing the effectiveness of the system to cope with multiple activity released throughout the ABSCE that may occur during a LOCA. Such coverage is accomplished by utilizing the normal ventilation ducting to draw outside air inleakage from any point along the secondary containment enclosure to the fuel handling and waste disposal areas.
(2) Accident indication signals are utilized to bring the ABGTS into operation to assure that the system functions when needed to mitigate accident effects.
Accidents in which this system is needed to preserve safety are automatically detected by at least one of the three instrumentation sets used to generate accident signals that result in system startup.
(3) System startup reliability is very high. The practice of allowing the automatic startup of both full capacity trains in the system gives greater assurance that one train of equipment functions upon receipt of an accident signal.
(4) The method adopted to establish and keep the negative pressure level within this secondary containment enclosure minimizes the time needed to reach the desired pressure level. Initially, the full capacity of the ABGTS fans is utilized for this purpose. After reaching the desired operating level, the system control module allows outside air to enter the air flow network just upstream of the fan at a rate to keep the fans operating at full capacity with the enclosed volume at the desired negative pressure level. In this situation, the amount of air withdrawn from the enclosed volume is equal to the amount of outside air inleakage through the ABSCE. In addition, two vacuum breaker dampers in series are provided to admit outside air in case the modulating dampers fail.
(5) The ABSCE is maintained at a slightly negative pressure to reduce the amount of unprocessed air escaping from this secondary containment enclosure to the atmosphere to insignificant quantities. In addition, this negative pressure level is less than that which is maintained within the annulus; such that, any air leakage between the Auxiliary Building and the Shield Building is from the Auxiliary Building into the Shield Building.
(6) The Train A and Train B air cleanup units are sufficiently separated from each other to eliminate the possibility of a single failure destroying the capability to process Auxiliary Building air prior to its release to the atmosphere. Two concrete walls and a distance of more than 80 feet separate the two trains.
The use of separate trains of the emergency power system to drive the air cleanup trains gives further assurance of proper equipment separation.
The review of the ABGTS conducted to determine its conformance with Regulatory Guide 1.52 has shown that this system, designed prior to issuance of the guide, is in 6.2.3-20 Design Evaluation
WATTS BAR WBNP-112 general agreement with its requirements. Details on compliance with Regulatory Guide 1.52 are given in Table 6.5-2.
The performance analysis conducted to verify that the ABGTS has the required accident mitigation capabilities has shown that the system flow rate is sized properly to handle all expected outside air inleakage at a 1/4-inch water gauge negative pressure differential. This indicates that the nominal flow rate of 9000 cfm is sufficient to assure an adequate margin above the expected ABSCE inleakage (ACU filters are replaced as needed to maintain a minimum flow capability of 9300 cfm under surveillance instructions).
The performance analysis evaluated the capability of the ABGTS to reach and maintain a negative pressure of 1/4-inch water gauge with respect to the outside within the boundaries of the ABSCE. The following was utilized in the analysis:
(1) Leakage into the ABSCE is proportional to the square root of the pressure differential.
(2) Only one air cleanup unit in the ABGTS operates at the rated capacity.
(3) The air cleanup unit fan begins to operate 30 seconds after the initiation of an ABI signal.
(4) The initial static pressure inside the ABSCE is conservatively considered to be atmospheric pressure, although the ABSCE is under a negative pressure during normal operation.
(5) The effective pressure head due to wind equals 1/8-inch water gauge.
(6) Initial average air temperature inside the ABSCE equals 140°F.
(7) Atmospheric temperature and pressure are 70°F and 14.4 psia, respectively.
(8) ABSCE isolation dampers/valves close within 30 seconds after receiving an ABI signal.
(9) The non-safety-related general ventilation and fuel handling area exhaust fans are designed to shut down automatically following a LOCA. Each fan is provided with a safety related Class 1E primary circuit breaker and a safety related Class 1E shunt trip isolation switch which is tripped by a signal of the opposite train from that for the primary circuit breaker to ensure that power is isolated from the fan.
The analysis utilizes the first law of thermodynamics and perfect gas relations in an iterative approach to determine temperature and pressure changes in the ABSCE.
Heat sources and sinks (ESF equipment room coolers) are considered.
Design Evaluation 6.2.3-21
WATTS BAR WBNP-112 The results obtained indicate that the ABGTS has the capability to reach and maintain a negative pressure differential of 0.25 inches water gauge within four minutes of the receipt of an ABI signal.
The system contains sufficient air cleanup facilities to keep the contributions to the site boundary and LPZ dosage arising from Auxiliary Building air releases to small fractions of the 10 CFR 100 guideline values. This part of the analysis is presented and evaluated in Chapter 15.
6.2.3.3.4 Tritium Production Core Evaluation (Unit 1 Only)
The effects of converting WBN to a Tritium Production Core (TPC) on the Secondary Containment design has been evaluated. The evaluation includes the effect of adding a leading edge flow meter (LEFM) into the main feedwater piping and the effect of uprating the plant nominal power level by 1.4%.
Secondary containment is designed to have the capability to control the atmosphere within the secondary containment and contiguous areas during normal operation and during plant upset conditions. As explained in UFSAR Section 6.2.1.3.12, the current licensing basis mass and energy release bounds that of the TPC; therefore, the conversion to a TPC will not have any effect on the secondary containment functional design.
6.2.3.4 Test and Inspections 6.2.3.4.1 Emergency Gas Treatment System (EGTS)
Preoperational testing of the EGTS was conducted to verify that the Shield Building and the EGTS had the capabilities needed to keep LOCA generated activity releases from the affected reactor unit at or below limits specified in 10 CFR 100. Included in the scope of testing were functional tests on all system instrumentation, controls, and alarms. The tests were structured to accomplish the following:
(1) Verification that Shield Building infiltration was less than or equal to the design value at the design negative pressure level for post-accident conditions.
(2) Verification of the system capability to establish and maintain the proper negative pressure level in the annulus.
(3) Verification that the air cleanup units met requirements specified in Regulatory Guide 1.52. Refer to Section 6.5.1.4.1 for further information related to tests applicable to the air cleanup units.
(4) Verification of proper operation of all system components, instrumentation, alarms, and data displays.
The periodic test program for the EGTS fans and air cleanup units is described in the Technical Specifications. A periodic test is performed once every 18 months to verify that the EGTS can maintain the annulus at a negative pressure within the instrument 6.2.3-22 Test and Inspections
WATTS BAR WBNP-112 deadband immediately above and below the nominal design value. This test also verifies that the Shield Building inleakage rate to the annulus is less than or equal to 250 cfm at the nominal design value. A verification of system flow capacity and Shield Building inleakage rates at the specified negative pressure is adequate to confirm that the calculated depressurization time is conservative. The EGTS fans start within 30 seconds following the initiation of a containment isolation phase A signal.
6.2.3.4.2 Auxiliary Building Gas Treatment System (ABGTS)
Preoperational testing of the ABGTS was conducted to verify that the ABGTS has the capabilities needed to reduce radioactive releases from the ABSCE to the environment during an accident to levels sufficiently low to keep the site boundary dose rates below the requirements of 10 CFR 100. Included in the test scope were functional tests on all system instrumentation, controls, and alarms. The tests were structured to accomplish the following:
(1) Verification of the system startup and control capabilities, considering a single operating component failure.
(2) Verification of the capability of the air flow control modules to create and maintain a negative pressure within the ABSCE.
(3) Verification that ABSCE infiltration rate was less than or equal to the design value at the design negative pressure level considering a postulated failure of a non-safety related component.
(4) Verification that the air cleanup units met the requirements specified in Regulatory Guide 1.52. Refer to Section 6.5.1.4.2 for further information related to tests applicable to the air cleanup units.
The periodic test program for the ABGTS fans and air cleanup units is described in the Technical Specifications. A periodic test is performed to verify that the ABGTS can maintain the ABSCE at a negative pressure between -0.25 and -0.5 inches of water with respect to atmospheric pressure. This test also verifies that the ABSCE vacuum relief flow rate is greater than or equal to 1370 cfm while the ABSCE is being maintained at the negative pressure described above. A verification of system flow capacity and ABSCE vacuum relief flow rate at the specified negative pressure is adequate to confirm that the calculated depressurization time is conservative.
6.2.3.5 Instrumentation Requirements 6.2.3.5.1 Emergency Gas Treatment System (EGTS)
The air flow control instrumentation requirements for the EGTS are described in Section 6.2.3.2.2. Instrumentation associated with the air cleanup units is discussed in Section 6.5.1.5.1. The logic, controls, and instrumentation of this engineered safety feature system are such that a single failure of any component does not result in the loss of functional capability for the system.
Instrumentation Requirements 6.2.3-23
WATTS BAR WBNP-112 6.2.3.5.2 Auxiliary Building Gas Treatment System (ABGTS)
Instrumentation required for the air flow control modules and air cleanup units are discussed in Section 6.2.3.2.3. Instrumentation associated with the air cleanup units is discussed in Section 6.5.1.5.2. The logic, controls, and instrumentation of this engineered safety feature system are such that a single failure of any component does not result in the loss of functional capability for the system.
REFERENCES None 6.2.3-24 Instrumentation Requirements
WATTS BAR WBNP-112 Table 6.2.3-1 Dual Containment Characteristics (Page 1 of 2)
I. Secondary Containment Design Information Shield Bldg. ABSCE (Incl. 2 x Shield Bldg., 2 x Contmt., AB and CDWE Bldg.)
A. Free Volume (ft3) 3.96 x 105 6.9 x 106 B. Pressure (in. wg)#
Normal Operation -5.0 -0.25 Post-Accident -0.5 -0.25 C. Leak Rate at Post- Accident Pressure (%/day) 91 165.5 D. Exhaust Fans Normal Operation Number 4 (2/reactor unit)* 6**
Type centrifugal centrifugal Post-Accident Operation Number 2*** 2****
Type centrifugal centrifugal E. Filters: Refer to Table 6.5-5 II. Transient Analysis A. Initial Conditions
- 1. Pressure = 14.4 psig
- 2. Annulus temperature = 50°F
- 3. Outside air temperature = 0°F
- 4. Thickness of secondary containment wall = 36 in.
- 5. Thickness of steel containment vessel = ranging from 0.8125 to 1.50 inches
- Annulus vacuum control subsystem
- Auxiliary Building general exhaust (2/unit) and fuel handling area exhaust (2)
- EGTS
- ABGTS
- Due to instrument locations and inaccuracies, the actual setpoints are more negative than the required values shown.
Instrumentation Requirements 6.2.3-25
WATTS BAR WBNP-112 Table 6.2.3-1 Dual Containment Characteristics (Page 2 of 2)
II. Transient Analysis (continued)
B. Thermal Characteristics
- 1. Primary containment wall
- a. Total expansion = 2000 ft3 Pressure expansion = 766 ft3 Temperature expansion = 1234 ft3
- b. Thermal conductivity = 31 Btu/hr-ft-°F
- c. Heat capacity = 0.111 Btu/lb-°F
- 2. Secondary containment wall
- a. Thermal conductivity = 1.6 Btu/hr-ft-°F
- b. Heat capacity = 0.22 Btu/lb-°F
- 3. Heat transfer coefficients
- a. Primary containment atmosphere to primary containment wall = 400 Btu/hr-ft2-°F
- b. Primary containment wall to secondary containment atmosphere = 0.19 (T)1/3 Btu/hr-ft2-°F
- c. Secondary containment wall to secondary containment atmosphere = 0.19 (T)1/3 Btu/hr-ft2-°F
- d. Primary containment emissivity = 0.90
- e. Secondary containment emissivity = 0.90 6.2.3-26 Instrumentation Requirements
Instrumentation Requirements WATTS BAR Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System (Page 1 of 17)
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS
- 1. EGTS ACU Fans Draws air from the - Stops running - Electrical Low flow alarm in Reduction of flow None (See Remarks) Redundant fan starts on A-A & B-B annulus to maintain - Does not run Failure the MCR from annulus and low flow signal from failed negative pressure in temporary reduction fan and train.
the annulus during - Mechanical in annulus negative design basis events Failure pressure Both trains of the EGTS system start on receipt of a Phase A isolation signal.
However, operators will align the system to single train operation after a period of time.
- 2. EGTS ACU Filters air to remove - Filters leak - Defective filters High radiation High radiation in None (See remarks) Periodic testing of EGTS A-A & B-B airborne particulates - Filters become levels indicated in shield building ACUs is conducted in and vapors from the loaded - High levels of the MCR from exhaust vent. accordance with R.G. 1.52 annulus during design radioactivity shield building to verify leak tightness of basis events contamination exhaust vent HEPA and charcoal bank efficiencies. High radiation
- Large quantities levels are indicated in the of particulates MCR for operators to start the redundant ACU, if necessary.
- 3. Containment Isolate annulus Open - Electrical Valve position None (See Remarks) None (See Remarks) Redundant valve in series annulus vacuum vacuum control fans Failure indication light in with failed valve provides control fan suction from EGTS during the MCR isolation function.
isolation valves ACU operation - Mechanical failure 1-FCV-65-52 1-FCV-65-53 2-FCV-65-4 2-FCV-65-5 6.2.3-27 WBNP-112
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System 6.2.3-28 WATTS BAR (Page 2 of 17)
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS
- 4. B train isolation Provide decay heat Open (ACU A-A is - Electrical Valve position Parallel flow path to None (See Remarks) Additional flow path is valves at EGTS removal cooling flow in operation) failure indication light in ACU A-A is open available which causes no Train A suction path for A-A ACU the MCR adverse effect.
1-FCV-65-8 when B-B ACU is - Mechanical (Unit 1 in LOCA) operating for Unit 1 Failure (valve open by Open (ACU A-A - Electrical Valve position If valves None (See Remarks) Valve on Fan A-A operator action) has not operated Failure indication light in 0-FCV-65-28A and discharge side and B-B is the MCR -28B are open, (0-FCV-65-24) closes operating) - Mechanical there will be when ACU A-A is in Failure negative pressure standby and will prevent on ACU A-A by backflow.
suction ACU fan B-B.
Closed (ACU A-A - Electrical Valve position None (See None (See Remarks) Operator will return to has operated and Failure indication light in Remarks) using ACU A-A.
is on stand-by and the MCR B-B is operating) - Mechanical An additional flow path is Failure available by opening 1-FCV-65-10, 0-FCV-65-28A and 0-FCV-65-28B.
Instrumentation Requirements WBNP-112
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System Instrumentation Requirements WATTS BAR (Page 3 of 17)
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS 4a. B train isolation Provide decay heat Open (ACU A-A is - Electrical Valve position Parallel flow path to None (See Remarks) Additional flow path is valves at EGTS removal cooling flow in operation) Failure indication light in the ACU A-A is open available which causes no Train A suction path for A-A ACU MCR adverse effect.
2-FCV-65-7 when B-B ACU is - Mechanical (Unit 2 in LOCA) operating for Unit 2 Failure (valve opened by operator action)
Open (ACU A-A - Electrical Valve position If valves None (See Remarks) Valve on Fan A-A has not operated Failure indication light in 0-FCV-65-28A and discharge side and B-B is the MCR -28B are open, (0-FCV-65-24) closes operating) - Mechanical there will be when ACU A-A is in Failure negative pressure standby and will prevent on ACU A-A by backflow.
suction ACU fan B-B.
Closed (ACU A-A - Electrical Valve position None (See None (See Remarks) Operator will return to has operated and Failure indication light in Remarks) using ACU A-A.
is on stand-by and the MCR B-B is operating) - Mechanical An additional flow path is Failure available by opening 2-FCV-65-9, 0-FCV-65-28A and 0-FCV-65-28B.
6.2.3-29 WBNP-112
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System 6.2.3-30 WATTS BAR (Page 4 of 17)
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS
- 5. A train isolation Provide decay heat Open (ACU B-B is - Electrical Valve position Parallel flow path to None (See Remarks) Additional flow path is valves at EGTS removal cooling path in operation) failure indication light in the ACU B-B is open available which causes no Train B suction for B-B ACU when A-A MCR adverse effect.
1-FCV-65-51 ACU is operating for - Mechanical (Unit 1 in LOCA) Unit 1 (valve opened failure by operator action)
Open (ACU B-B - Electrical Valve position If valves None (See Remarks) Valve on Fan B-B has not operated failure indication light in 0-FCV-65-47A and discharge side and A-A is the MCR - 47B are open, 0-FCV-65-43 closes operating) - Mechanical there will be when ACU B-B is in failure negative pressure standby and will prevent on ACU B-B by backflow.
suction ACU fan A-A.
Closed (ACU B-B - Electrical Valve position None (See None (See Remarks) Operator will return to has operated and failure indication light in Remarks) using ACU B-B.
is on Stand-by the MCR and A-A is - Mechanical An additional flow path is operating) failure available by opening 1-FCV-65-30, 0-FCV-65-47A and 0-FCV-65-47B.
Instrumentation Requirements WBNP-112
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System Instrumentation Requirements WATTS BAR (Page 5 of 17)
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS 5a. A train isolation Provide decay heat Open (ACU B-B is - Electrical Valve position Parallel flow path to None (See Remarks) Additional flow path is valves at EGTS removal cooling path in operation) failure indication light in the ACU B-B is open available which causes no Train B suction for B-B ACU when A-A MCR adverse effect.
2-FCV-65-50 ACU is operating for - Mechanical (Unit 2 in LOCA) Unit 2 (valve opened failure by operator action)
Open (ACU B-B - Electrical Valve position If valves None (See Remarks) Valve on Fan B-B has not operated failure indication light in 0-FCV-65-47A and discharge side and A-A is the MCR - 47B are open, 0-FCV-65-43 closes operating) - Mechanical there will be when ACU B-B is in failure negative pressure standby and will prevent on ACU B-B by backflow.
suction ACU fan A-A.
Closed (ACU B-B - Electrical Valve position None (See None (See Remarks) Operator will return to has operated and failure indication light in Remarks) using ACU B-B.
is on Stand-by the MCR and A-A is - Mechanical An additional flow path is operating) failure available by opening 2-FCV-65-29, 0-FCV-65-47A and 0-FCV-65-47B.
6.2.3-31 WBNP-112
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System 6.2.3-32 WATTS BAR (Page 6 of 17)
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS
- 6. Isolation valve at Isolation control valve Closed (ACU A-A - Electrical Low flow alarm and Momentary decrease None (See Remarks) Redundant ACU Fan B-B EGTS Train A that opens on a is in operation) failure valve position in flow starts on low flow signal suction, containment isolation indication light in the from Fan A-A and 1-FCV-65-10 signal so that the - Mechanical MCR Valve 1-FCV-65-30 is (Unit 1 in LOCA) EGTS can exhaust air failure opened. The fan starting from the annulus. It signal is independent of also isolates Train A valve failure.
ACU during normal plant operation.
Closed (both - Electrical Low flow alarm and Momentary None (See Remarks) Train B ACU continues to Trains A-A and failure valve indication light decrease in flow operate with Valve B-B ACUs are in the MCR 1-FCV-65-30 open.
operating) - Mechanical failure Open (Train B-B is - Electrical Valve position Open backflow path None (See Remarks) Flow Control Valve operating. A-A is failure indication light in to ACU A-A 0-FCV-65-24 and not operating and the MCR Backdraft Damper has never - Mechanical 0-65-524 close when operated or has failure ACU A-A is in standby operated and and will prevent stopped.) backflow.
Instrumentation Requirements WBNP-112
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System Instrumentation Requirements WATTS BAR (Page 7 of 17)
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS 6a. Isolation valve at Isolation control valve Closed (ACU A-A - Electrical Low flow alarm and Momentary decrease None (See Remarks) Redundant ACU Fan B-B EGTS Train A that opens on a is in operation) failure valve position in flow starts on low flow signal suction, containment isolation indication light in the from Fan A-A and 2-FCV-65-9 signal so that the - Mechanical MCR Valve 2-FCV-65-29 is (Unit 2 in LOCA) EGTS can exhaust air failure opened. The fan starting from the annulus. It signal is independent of also isolates Train A valve failure.
ACU during normal plant operation.
Closed (both - Electrical Low flow alarm and Momentary None (See Remarks) Train B ACU continues to Trains A-A and failure valve position decrease in flow operate with Valve B-B ACUs are indication light in 2-FCV-65-29 open.
operating) - Mechanical the MCR failure Open (Train B-B is - Electrical Valve position Open backflow path None (See Remarks) Flow Control Valve operating. A-A is failure indication light in to ACU A-A 0-FCV-65-24 and not operating and the MCR Backdraft Damper has never - Mechanical 0-65-523 close when operated or has failure ACU A-A is in standby operated and and will prevent stopped.) backflow.
6.2.3-33 WBNP-112
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System 6.2.3-34 WATTS BAR (Page 8 of 17)
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS
- 7. Isolation valves at Isolation control valve Closed (ACU B-B -Electrical failure Low flow alarm and Momentary decrease None (See remarks) Redundant ACU Fan A-A EGTS Train B that opens on a is in operation) valve position in flow starts on low flow signal suction, containment isolation - Mechanical indication light in the from Fan B-B and Valve 1-FCV-65-30 signal so that the failure MCR 1-FCV-65-10 is opened.
(Unit 1 in LOCA) EGTS can exhaust air The fan starting signal is from the annulus. It independent of valve also isolates Train B failure.
ACU during normal plant operation.
Closed (both - Electrical Low flow alarm and Momentary None (See remarks) Train A ACU continues to Trains A-A and failure valve position decrease in flow operate with Valve B-B ACUs are indication light in 1-FCV-65-10 open.
operating.) - Mechanical the MCR failure Open (Train A-A is - Electrical Valve position Open backflow path None (See remarks) Flow Control Valve operating. B-B is failure indication light in to ACU B-B 0-FCV-65-43 and not operating and the MCR backdraft damper has never - Mechanical 0-65-526 close when operated or has failure ACU B-B is in standby operated and and will prevent stopped.) backflow. Also, the additional flow paths will not cause an adverse effect.
Instrumentation Requirements WBNP-112
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System Instrumentation Requirements WATTS BAR (Page 9 of 17)
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS 7a. Isolation valves at Isolation control valve Closed (ACU B-B - Electrical Low flow alarm and Momentary decrease None (See remarks) Redundant ACU Fan A-A EGTS Train B that opens on a is in operation) failure valve position in flow starts on low flow signal suction, containment isolation indication light in the from Fan B-B and Valve 2-FCV-65-29 signal so that the - Mechanical MCR 2-FCV-65-9 is opened.
(Unit 2 in LOCA) EGTS can exhaust air failure The fan starting signal is from the annulus. It independent of valve also isolates Train B failure.
ACU during normal plant operation.
Closed (both - Electrical Low flow alarm and Momentary None (See remarks) Train A ACU continues to Trains A-A and failure valve position decrease in flow operate with Valve B-B ACUs are indication light in 2-FCV-65-9 open.
operating.) - Mechanical the MCR failure Open (Train B-B is - Electrical Valve position Open backflow path None (See remarks) Flow Control Valve operating. A-A is failure indication light in to ACU A-A 0-FCV-65-24 and not operating and the MCR backdraft damper has never - Mechanical 0-65-525 close when operated or has failure ACU B-B is in standby operated and and will prevent stopped.) backflow. Also, the additional flow paths will not cause an adverse effect.
- 8. EGTS fan Isolates EGTS fan One damper fails - Electrical Low flow alarm and Loss of flow through None (See remarks) Redundant fan starts on discharge isolation from duct distribution closed (EGTS fan failure valve position the affected EGTS low flow signal from the valves system when EGTS is operating) indication light in the train affected train. Fan 0-FCV-65-24 fan is on standby - Mechanical MCR starting signal is 0-FCV-65-43 failure independent of valve failure.
6.2.3-35 WBNP-112
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System 6.2.3-36 WATTS BAR (Page 10 of 17)
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS
- 9. Shield building Open air path for One damper fails - Electrical Damper position None (See Remarks) None (See Remarks) Damper in parallel flow exhaust isolation EGTS exhaust to be closed failure indication light in the path is open.
dampers discharged to either MCR 1-FCO-65-26 shield building vent - Mechanical 1-FCO-65-27 and recirculated air failure 2-FCO-65-45 flow to either annulus 2-FCO-65-46 10 EGTS inlet flow elements abandoned in place (1-FE-65-54 and 2-FE-65-3).
11 Shield building Exhaust flow elements abandoned in place (1-FE-65-84 and -85, 1-FE-65-78, 2-FE-65-84 and -85, 2-FE-65-78)
Instrumentation Requirements WBNP-112
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System Instrumentation Requirements WATTS BAR (Page 11 of 17)
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS
- 12. Back draft Prevent backflow Damper closed - Mechanical Low flow alarm Momentary decrease None (See Remarks) Redundant ACU Fan B-B dampers through Train A ACU (Train A ACU is in failure indication light in the in flow from annulus starts on low flow from 0-65-523 when Train B ACU is in operation and MCR Train A-A. Fan starting 0-65-524 operation Train B ACU is in signal is independent of standby) damper failure.
Damper closed - Mechanical Low flow alarm None (See None (See Remarks) Train B ACU continues to (Both Train A & failure indication light in Remarks) operate and Train A will Train B are the MCR be turned off by operator.
operational)
- 13. Back draft Prevent backflow Damper closed - Mechanical Low flow alarm Momentary decrease None (See Remarks) Redundant ACU Fan A-A dampers through Train B ACU (Train B ACU is in failure indication light in the in flow from annulus starts on low flow from 0-65-525 when Train A ACU is in operation and MCR Train B-B. Fan starting 0-65-526 operation Train A ACU is in signal is independent of standby) damper failure.
Damper closed - Mechanical Low flow alarm None (See None (See Remarks) Train A ACU continues to (Both Train A & failure indication light in Remarks) operate and Train B will Train B are the MCR be turned off by operator.
operational) 6.2.3-37 WBNP-112
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System 6.2.3-38 WATTS BAR (Page 12 of 17)
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS
- 14. Modulating Modulates EGTS flow Damper closed, - Mechanical Pressure differential With the worst case None. The elevated Off-site and control room dampers released to outside open or improper linkage failure is indicated in the PCO single failure, 957 cfm (832 cfm for radiological dose 1-PCO-65-80 atmosphere, modulation.The MCR to detect the the EGTS maintains U2) short term / 694 analyses demonstrate 1-PCO-65-82 controlling to the worst case PCO - Control Loop -2.1 (-1.88 for U2) annulus -P at -2.1 (- cfm (604 cfm for U2) that the offsite and 1-PCO-65-88 required annulus single failure is Failure of one w.g. annulus 1.88 for U2) w.g. long term EGTS control room dose results 1-PCO-65-89 negative pressure such that either Train of PCOs. -P. However, the (steady state) during exhaust flow associate remain below the 2-PCO-65-80 1(2)-PCO-65-80 worst case PCO the short term, which with the worst case regulatory limits, when 2-PCO-65-82 or -82 fail open to failure has been is acceptable since it PCO single failure the elevated EGTS 2-PCO-65-88 the shield building analyzed to exist is more negative than mode is addressed in exhaust flows associated 2-PCO-65-89 stack, and the with both trains of the Remarks. with the worst case PCO opposite train EGTS fans running -1.45 w.g. controller single failure scenario are PCOs still for the first one to setpoint. When one considered.
modulate and two hours after EGTS fan is stopped attempt to event initiation; and between one and two maintain annulus - then one fan running hours by operator P at the thereafter due to action, the resulting
-1.45 w.g. control operator action to configuration setpoint. This shut off one EGTS maintains annulus single failure fan. -P at -1.60 (-1.48 scenario takes the for U2) w.g., which is short term annulus still slightly more steady state -P to negative than
-2.1 (-1.88 for -1.45 w.g.
U2) w.g.
(i.e., failed PCO train with open flow path to the shield building stack and Instrumentation Requirements non-failed PCO train with open recirculation flow path to the annulus and two fans operating.)
WBNP-112
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System Instrumentation Requirements WATTS BAR (Page 13 of 17)
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS
- 15. Isolation valves Isolates EGTS One valve closed - Electrical Valve position One of the two None (See Remarks) Redundant flow path is 1-PCV-65-81 ductwork from outside when EGTS is in failure indication light in the parallel flow paths is available 1-PCV-65-83 atmosphere and ring operation MCR lost 1-PCV-65-86 header during normal - Mechanical 1-PCV-65-87 plant operation Failure 2-PCV-65-81 2-PCV-65-83 2-PCV-65-86 2-PCV-65-87
- 16. Isolation valves Valves open to remove One valve opens -Electrical failure Valve position None (See Remarks) None (See Remarks) Redundant isolation 0-FCV-65-28A decay heat in the idle when bypass indication light in the valves 0-FCV-65-28B train ACU cooling is not in - Mechanical MCR operation Failure One valve closed - Electrical Valve position None (See Remark) None (See Remarks) Bypass cooling provision when bypass failure indication light in will not be used unless cooling is in the MCR ACU fails and enough operation - Mechanical heat is generated by failure radioactivity collected on HEPA and charcoal adsorber to raise the charcoal bed temperature significantly.
Therefore, a second failure (closed isolation valve) need not be postulated.
6.2.3-39 WBNP-112
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System 6.2.3-40 WATTS BAR (Page 14 of 17)
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS
- 17. Isolation valves Valves open to remove One valve opens - Electrical Valve position None (See Remarks) None (See Remarks) Redundant isolation 0-FCV-65-47A decay heat in the idle when bypass failure indication light in the valves 0-FCV-65-47B train ACU cooling is not in MCR operation - Mechanical failure One valve closed - Electrical Valve position None (See Remarks) None (See Remarks) Bypass cooling provision when bypass failure indication light in will not be used unless cooling is in the MCR ACU fails and enough operation - Mechanical heat is generated by failure radioactivity collected on HEPA and charcoal adsorber to raise the charcoal bed temperature significantly.
Therefore, a second failure (closed isolation valve) need not be postulated.
- 18. Flow elements Opens decay heat No signal sent - Electrical Valve position None (See Remarks) None (See Remarks) Bypass cooling provision 0-FS-65-31A/B removal isolation failure indication light in the will not be used unless 0-FS-65-55A/B valves to the operating MCR ACU fails and enough ACU when no flow is heat is generated by sensed at the idle ACU radioactivity collected on HEPA and charcoal adsorber to raise the charcoal bed temperature Instrumentation Requirements significantly. Therefore, a second failure (closed isolation valve) need not be postulated.
WBNP-112
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System Instrumentation Requirements WATTS BAR (Page 15 of 17)
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS
- 19. Flow elements Starts EGTS standby No signal sent - Electrical Valve position Momentary decrease None (See Remarks) Bypass cooling provision 0-FS-65-31B/A ACU unit upon loss of failure indication light in the in flow from annulus will not be used unless 0-FS-65-55B/A flow in normally MCR ACU fails and enough operating ACU heat is generated by radioactivity collected on HEPA and charcoal adsorber to raise the charcoal bed temperature significantly.
Therefore, a second failure (closed isolation valve because signal not sent) need not be postulated.
- 20. Flow elements Shuts off relative No signal sent - Electrical Low flow and high Humidity heater may None (See Remarks) The EGTS fan can be 0-FS-65-25A/B humidity heater on low failure temperature alarms stay on after EGTS stopped either by 0-FS-65-44A/B air flow and alarm in in the MCR fan stops operators action or fan the MCR failure, which is a single failure; the other EGTS fan is available to function. The heater requires two signals to operate: one from flow switch and one from temperature switch.
Therefore, heater not receiving the signal need not be assumed.
6.2.3-41 WBNP-112
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System 6.2.3-42 WATTS BAR (Page 16 of 17)
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS
- 21. Flow elements Opens decay heat No signal sent - Electrical Valve position None (See Remarks) None (See Remarks) Bypass cooling provision 0-FS-65-25B/A removal isolation failure indication light in the will not be used unless 0-FS-65-44B/A valves on idle ACU MCR ACU fails and enough when high flow is heat is generated by sensed at the radioactivity collected on operating ACU HEPA and charcoal adsorber to raise the charcoal bed temperature significantly.
Therefore, a second failure (closed isolation valve because signal not sent) need not be postulated.
22 Train A Provides Class 1E Loss of or Diesel generator Alarm and Loss of redundancy None (See Remarks) Redundant train of EGTS Emergency Power diesel-backed power inadequate failure; bus fault indication in the in EGTS exhaust is turned on by automatic supply to active Voltage (Train A); MCR flow paths and manual actions on components of Train A operator error loss of fan airflow, or of EGTS annulus -P, which ensures that the EGTS safety functions are continued to be performed.
23 Train B Provides Class 1E Loss of or Diesel generator Alarm and Loss of redundancy None (See Remarks) Redundant train of EGTS Emergency Power diesel-backed power inadequate failure; bus fault indication in the in EGTS exhaust is turned on by automatic supply to active Voltage (Train B); MCR flow paths and manual actions on components of Train B operator error loss of fan airflow, or Instrumentation Requirements of EGTS annulus -P, which ensures that the EGTS safety functions are continued to be performed.
WBNP-112
Table 6.2.3-2 Failure Modes and Effects Analysis Emergency Gas Treatment System Instrumentation Requirements WATTS BAR (Page 17 of 17)
METHOD OF EFFECT EFFECT COMPONENT FAILURE POTENTIAL FAILURE ON ON IDENTIFICATION FUNCTION MODE CAUSE DETECTION SYSTEM PLANT REMARKS 24 Deluge Valve Floods the carbon Spurious - Electrical Local and MCR None (See None (See Remarks) ACU will not be flooded 0-FCV-26-175 absorbers in the event actuation failure alarms on water Remarks) since the fusible links on of fire discharge the spray heads will be
- Mechanical closed due to absence of failure heat.
24a Deluge System Floods the carbon Spurious - Fusible Link None Loss of redundancy None (See Remarks) Opposite train ACU is Piping/Heads on absorbers in the event actuation Failure in EGTS unaffected and remains Train A of fire available.
- Piping Failure 25 Deluge Valve Floods the carbon Spurious - Electrical Local and MCR None (See None (See Remarks) ACU will not be flooded 0-FCV-26-179 absorbers in the event actuation failure alarms on water Remarks) since the fusible links on of fire discharge the spray heads will be
- Mechanical closed due to absence of failure heat.
25a Deluge System Floods the carbon Spurious - Fusible Link None Loss of redundancy None (See Remarks) Opposite train ACU is Piping/Heads on absorbers in the event actuation Failure in EGTS unaffected and remains Train B of fire available.
- Piping Failure 6.2.3-43 WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 1 of 27) 6.2.3-44 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 1 Auxiliary Building De-energizes solenoid Signal fails. Train A vital ac bus MCR indication of Loss of None. (See Train A and Train B ABI initiating Isolation (ABI) valves to close failure; Relay VKA1 only one train redundancy in Remarks) signals are derived from signal Train A associated dampers failure; Train A ABGTS fan starting ABSCE isolation independent (train-separated) and establish AB initiating signal and one train of and in ABGTS until qualified devices.
secondary containment (Phase A containment ABSCE dampers operator starts enclosure; stops AB isolation, high rad in closing. Train A ABGTS Either train signal is sufficient to general ventilation refueling area, manually from stop all AB general vent supply fans; starts various high temp. in Aux. MCR, after and exhaust fans and fuel handling ESF room coolers; Building general ascertaining that area exhaust fans. SInce ABSCE starts ABGTS fans to supply duct) failure. Train B ABI signal dampers are arranged in series, maintain negative is not spurious. either trains actuation is adequate pressure in the ABSCE to establish the ABSCE boundary.
and remove contaminants from the ABSCE air prior to discharge to atmosphere.
Starts Train A ABGTS, Same as Same as above. Same as above. Same as above. None. (See Only Train B ABGTS will start and closes Train A ABSCE above. Remarks). only Train B ABSCE isolation isolation dampers, dampers will close. Train A stops Train A containment purge air supply fan containment purge air and exhaust fan may be running, supply and exhaust and the Incore Instrument Room fans (Ref.5.28) suppy and exhaust fans will stop (both Train B). For conservatism, it is assumed that all exhaust fans are stopped. Preoperational and surveillance tests have shown that, in this configuration, the ABGTS is able to fulfill its safety functions.
Same as above. Spuriously Operator error, MCR indicating *Disrupts the None. (See Unnecessary isolation of ABSCE starts. spurious initiating lights on ABGTS normally operating Remarks) and actuation of ABGTS, as well Instrumentation Requirements signal (initiating signals start and ABSCE ventilation system, as disrupting the normally listed above) dampers closure. and starts safety- operating ventilation systems and related systems starting the ESF pump room and and components. area coolers.
- Interim U1 configuration: As a result of the changes made by DCN 56414, a spurious ABI signal would also result in a Containment Vent Isolation (CVI) signal.
WBNP-112 Dual Unit configuration: EDCR 55801 provides for a functional cross-tie between the two units which would cause a refueling unit CVI upon spurious ABI signal.
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 2 of 27)
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 2 Auxiliary Building De-energizes solenoid Signal fails. Train B vital ac bus MCR indication of Loss of None (See Train A and Train B ABI initiating Isolation (ABI) valves to close failure; Relay VKA1 only one train redundancy in Remarks) signals are derived from signal Train B associated dampers failure; Train B ABGTS fan starting ABSCE isolation independent (train-separated) and establish AB initiating signal (Phase and one train of and in ABGTS until qualified devices.
secondary containment A containment ABSCE dampers operator starts enclosure; stops AB isolation, high rad in closing. Train B ABGTS Either train signal is sufficient to general ventilation refueling area, high manually from stop all AB general vent supply fans; starts various temp. in Aux. Building MCR, after and exhaust fans and fuel handling ESF room coolers; general supply duct) ascertaining that area exhaust fans. SInce ABSCE starts ABGTS fans to failure. Train A ABI signal dampers are arranged in series, maintain negative is not spurious either trains actuation is adequate pressure in ABSCE and to establish the ABSCE boundary.
remove contaminants from the ABSCE air prior to discharge to atmosphere.
Starts Train B ABGTS, Same as Same as above. Same as above. Same as above. None. (See Only Train B ABGTS will start and closes Train B ABSCE above. Remarks). only Train B ABSCE isolation isolation dampers, dampers will close. Train B stops Train B containment purge air supply fan containment purge air and exhaust fan may be running, supply and exhaust and the Incore Instrument Room fans and stops the suppy and exhaust fans may be Incore Instrument running. For conservatism, it is Room supply and assumed that all exhaust fans are exhaust fans (Ref.5.28) stopped. Preoperational and surveillance tests have shown that, in this configuration, the ABGTS is able to fulfill its safety functions.
(See Section 8.3 for detail).
Same as above. Spuriously Operator error, MCR indicating *Disrupts the None. (See Unnecessary isolation of ABSCE starts. spurious initiating lights on ABGTS normally operating Remarks). and actuation of ABGTS, as well signal (initiating signals start and ABSCE ventilation systems as disrupting the normally listed above) dampers closure. and starts safety- operating ventilation systems and related systems starting the ESF pump room and and components area coolers.
WBNP-112
- Interim U1 configuration: As a result of the changes made by DCN 56414, a spurious ABI signal would also result in a Containment Vent Isolation (CVI) signal.
Dual Unit configuration: EDCR 55801 provides for a functional cross-tie between the two units which would cause a refueling unit CVI upon spurious ABI signal.
6.2.3-45
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 3 of 27) 6.2.3-46 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 3 ABGTS Exhaust Draws a portion of air in Fails to start or Mechanical failure; Indicating light in Loss of None. Handswitches for ABGTS Fans Fan A-A the ABSCE through an fails to run. Train A power failure; the MCR. redundancy in ABGTS Fan A-A and B-B in the MCR should air cleanup unit (ACU) Train A ABI signal ABGTS. B-B can normally be in the A-Auto position.
to remove radioactive (HS in A-Auto). perform the On an ABI signal, both fans start contaminants and functions of and the operator may stop one fan discharge into the maintaining and place its handswitch in the shield building exhaust the ABSCE at P-Auto (pull-out) position. This vent to maintain a a negative mode of operation is expected to negative pressure in pressure and occur after 30 minutes of two fan the ABSCE relative to removing operation. During an ABI, the fan the outside. contaminants. in the P-Auto mode will start automatically on insufficient negative pressure in the ABSCE relative to the outside. An alarm is provided for the condition when flow is inadequate 45 seconds after fan start.
Starts Spurious Train A ABI See "Remarks" Vacuum relief line None (See Ind. light in the MCR provides spuriously. signal (HS in A-Auto); column. dampers may open Remarks) indication to operator that fan is spurious low flow to prevent running. However, if only one signal from Fan B-B excessive negative ABGTS train starts when both fans after valid ABI signal pressure in ABSCE are in A-Auto or if the fan in P-Auto (HS in P-Auto). by admitting starts, the operator cannot outside air. determine whether the signal is valid or spurious (no detection of spurious operation). This is acceptable since there is no impact on plant safety without a second failure (e.g., failure of a vacuum relief damper).
Instrumentation Requirements See end of Table 6.2.3-3 for the effects of the potential ABGTS fan failures on the EGTSs ability to maintain the annulus -P more negative than that of the ABSCE.
WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 4 of 27)
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 4 ABGTS Exhaust Draws a portion of air in Fails to start or Mechanical failure; Indicating light in Loss of None. Handswitches for ABGTS Fans Fan B-B the ABSCE through an fails to run. Train B power failure; the MCR. redundancy in ABGTS Fan A-A and B-B, in the MCR should air cleanup unit (ACU) Train B ABI signal ABGTS. A-A can normally be in the A-Auto position.
to remove radioactive failure (HS in A-Auto). perform the On an ABI signal, both fans start contaminants and functions of and the operator may stop one fan discharge into the maintaining and place its handswitch in the shield building exhaust the ABSCE at P-Auto (pull-out) position. This vent to maintain a a negative mode of operation is expected to negative pressure in pressure and occur after 30 minutes of two fan the ABSCE relative to removing operation. During an ABI, the fan the outside. contaminants. in the P-Auto mode will start automatically on insufficient negative pressure in the ABSCE relative to the outside. An alarm is provided for the condition when flow is inadequate 45 seconds after fan start.
Starts Spurious Train B ABI See "Remarks" Vacuum relief line None. Ind. light in the MCR provides spuriously. signal (HS in A-Auto); column. dampers may open indication to operator that fan is spurious low flow to prevent running. However, if only one signal from Fan A-A excessive negative ABGTS train starts when both fans after valid ABI signal pressure in ABSCE are in A-Auto or if the fan in P-Auto (HS in P-Auto). by admitting starts, the operator cannot outside air. determine whether the signal is valid or spurious (no detection of spurious operation). This is acceptable since there is no impact on plant safety without a second failure (e.g., failure of a vacuum relief damper).
See end of Table 6.2.3-3 for the effects of the potential ABGTS fan failures on the EGTSs ability to maintain the annulus -P more negative than that of the ABSCE.
6.2.3-47 WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 5 of 27) 6.2.3-48 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 5 ABGTS Fan A-A Provides flowpath for Fails to open Mechanical failure. Alarm in the MCR Loss of None (See ABGTS Fan A-A Inlet and Outlet Inlet Damper ABGTS Exhaust Fan or stuck from 1-FS-30-146 redundancy in Remarks) Dampers 1-FCO-30-146A and 1-FCO-30-146B A-A. closed. ABGTS. 1-FCO-30-146B open on starting of associated fan and close when the fan stops.
ABGTS fan B-B provides redundancy.
Provides isolation of Fails to close Mechanical failure Alarm in the MCR None (See None (See Damper 146A provides ACU A-A when fan A-A or stuck open. from 1-FS-30-146 Remarks) Remarks) redundancy (both dampers fail is not running. closed).
6 ABGTS Fan A-A Provides flowpath for Fails to open Mechanical failure. Alarm in the MCR Loss of None (See ABGTS Fan A-A Inlet and Outlet Outlet Damper ABGTS Exhaust Fan or stuck from 1-FS-30-146 redundancy in Remarks) Dampers 1-FCO-30-146A and 1-FCO-30-146A A-A. closed. ABGTS. 1-FCO-30-146B open on starting of associated fan and close when the fan stops.
Provides isolation of Fails to close Mechanical failure. Alarm in the MCR None (See None (See Damper 146B provides ACU A-A when fan A-A or stuck open. from 1-FS-30-146 Remarks) Remarks) redundancy (both dampers fail is not running. closed).
7 ABGTS Fan B-B Provides flowpath for Fails to open Mechanical failure. Alarm in the MCR Loss of None (See ABGTS Fan B-B Inlet and Outlet Inlet Damper ABGTS Exhaust Fan or stuck from 2-FS-30-165 redundancy in Remarks) Dampers 2-FCO-30-157A and 2-FCO-30-157B B-B. closed. ABGTS. 2-FCO-30-157B open on starting of associated fan and close when the fan stops.
ABGTS fan A-A provides redundancy.
Instrumentation Requirements Provides isolation of Fails to close Mechanical failure. Alarm in the MCR Loss of None (See Damper 157A provides ACU B-B when fan B-B or stuck open from 2-FS-30-165 redundancy in Remarks) redundancy (both dampers fail is not running. ABGTS. closed).
WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 6 of 27)
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 8 ABGTS Fan B-B Provides flowpath for Fails to open Mechanical failure. Alarm in the MCR Loss of None (See ABGTS Fan B-B Inlet and Outlet Outlet Damper ABGTS Exhaust Fan or stuck from 2-FS-30-165 redundancy in Remarks) Dampers 2-FCO-30-157A and 2-FCO-30-146A B-B. closed. ABGTS. 2-FCO-30-157B open on starting of associated fan and close when the fan stops.
ABGTS fan A-A provides redundancy.
Provides isolation of Fails to close Mechanical failure. Alarm in the MCR Loss of None (See Damper 157B provides ACU B-B when fan B-B or stuck open from 2-FS-30-165 redundancy in Remarks) redundancy (both dampers fail is not running. ABGTS. closed).
9 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-30-137 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A (0-Train A signal to isolate Fuel or spuriously Train A ABI or high rad isolation of Fuel Damper FCO-30-137) and Train B (0-FCO-Handling Area Exhaust opens. in refueling area signal Handling Area 0-FCO-30-138 30-138) dampers, in series, are Fan A-A and to failure; HS failure to Exhaust Fan A-A. provides provided with non-safety control establish boundary for spring return from isolation and air. Loss of the non-safety related ABGTS. open to A-Auto. maintains the control air does not prevent the ABSCE. damper from closing.
Independence of Train A and Train B isolation signals is discussed in "Remarks" under items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
6.2.3-49 WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 7 of 27) 6.2.3-50 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 10 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-30-138 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A (0-Train B signal to isolate Fuel or spuriously Train B ABI or high rad isolation of Fuel Damper FCO-30-137) and Train B (0-FCO-Handling Area Exhaust opens. in refueling area signal Handling Area 0-FCO-30-137 30-138) dampers, in series, are Fan A-A and to failure; HS failure to Exhaust Fan A-A. provides provided with non-safety control establish boundary for spring return from isolation and air. Loss of the non-safety related ABGTS. open to A-Auto. maintains the control air does not prevent the ABSCE. damper from closing.
Independence of Train A and Train B isolation signals is discussed in "Remarks" under items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
11 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-30-140 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A (0-Train A signal to isolate Fuel or spuriously Train A ABI or high rad isolation of Fuel Damper FCO-30-140) and Train B (0-FCO-Handling Area Exhaust opens. in refueling area signal Handling Area 0-FCO-30-141 30-141) dampers, in series, are Fan B-B and to failure; HS failure to Exhaust Fan B-B. provides provided with non-safety control establish boundary for spring return from isolation and air. Loss of the non-safety related ABGTS. open to A-Auto. maintains the control air does not prevent the ABSCE. damper from closing.
Independence of Train A and Train B, isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed Instrumentation Requirements since the damper has no safety function to open for DBE mitigation.
WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 8 of 27)
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 12 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-30-141 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train A 125 Vdc power. Train A (0-Train B signal to isolate Fuel or spuriously Train B ABI or high rad isolation of Fuel Damper FCO-30-140) and Train B (0-FCO-Handling Area Exhaust opens. in refueling area signal Handling Area 0-FCO-30-140 30-141) dampers, in series, are Fan B-B and to failure; HS failure to Exhaust Fan B-B. provides provided with non-safety control establish boundary for spring return from isolation and air. Loss of the non-safety related ABGTS. open to A-Auto. maintains the control air does not prevent the ABSCE. damper from closing.
Independence of Train A and Train B, isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
13 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 2-FCO-30-21 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate AB or spuriously Train A ABI or high rad isolation of part of Damper (2-FCO-30-21) and Train B Gen Supply Fans 2A-A opens. in refueling area signal ductwork on Unit 2 2-FCO-30-22 (2-FCO-30-22) dampers, in series, and 2B-B and to failure; HS failure to side of AB. provides are provided with non-safety establish boundary for spring return from isolation and control air and both dampers fail ABGTS. open to A-Auto. maintains the closed on loss of control air.
ABSCE. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
6.2.3-51 WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 9 of 27) 6.2.3-52 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 14 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 2-FCO-30-22 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate AB or spuriously Train B ABI or high rad isolation of part of Damper (2-FCO-30-21) and Train B Gen Supply Fans 2A-A opens. in refueling area signal ductwork on Unit 2 2-FCO-30-21 (2-FCO-30-22) dampers, in series, and 2B-B and to failure; HS failure to side of AB. provides are provided with non-safety establish boundary for spring return from isolation and control air and both dampers fail ABGTS. open to A-Auto. maintains the closed on loss of control air.
ABSCE. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
15 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1-FCO-30-86 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate AB or spuriously Train A ABI or high rad isolation of part of Damper (1-FCO-30-86) and Train B Gen Supply Fans 1A-A opens. in refueling area signal ductwork on Unit 1 1-FCO-30-87 (1-FCO-30-87) dampers, in series, and 1B-B and to failure; HS failure to side of AB. provides are provided with non-safety establish boundary for spring return from isolation and control air and both dampers fail ABGTS. open to A-Auto. maintains the closed on loss of control air.
ABSCE. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE Instrumentation Requirements mitigation.
WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 10 of 27)
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 16 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1-FCO-30-87 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate AB or spuriously Train B ABI or high rad isolation of part of Damper (1-FCO-30-86) and Train B Gen Supply Fans 1A-A opens. in refueling area signal ductwork on Unit 1 1-FCO-30-86 (1-FCO-30-87) dampers, in series, and 1B-B and to failure; HS failure to side of AB. provides are provided with non-safety establish boundary for spring return from isolation and control air and both dampers fail ABGTS. open to A-Auto. maintains the closed on loss of control air.
ABSCE. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
17 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1-FCO-30-106 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate AB or spuriously Train A ABI or high rad isolation of part of Damper (1-FCO-30-106) and Train B Gen Supply Fans 1A-A opens. in refueling area signal ductwork on Unit 1 1-FCO-30-107 (1-FCO-30-107) dampers, in and 1B-B and to failure; HS failure to side of AB. provides series, are provided with establish boundary for spring return from isolation and non-safety control air and both ABGTS. open to A-Auto. maintains the dampers fail closed on loss of ABSCE. control air. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
6.2.3-53 WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 11 of 27) 6.2.3-54 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 18 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1-FCO-30-107 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate AB or spuriously Train B ABI or high rad isolation of part of Damper (1-FCO-30-106) and Train B Gen Supply Fans 1A-A opens. in refueling area signal ductwork on Unit 1 1-FCO-30-106 (1-FCO-30-107) dampers, in and 1B-B and to failure; HS failure to side of AB. provides series, are provided with establish boundary for spring return from isolation and non-safety control air and both ABGTS. open to A-Auto. maintains the dampers fail closed on loss of ABSCE. control air. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
19 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 2-FCO-30-108 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate AB or spuriously Train A ABI or high rad isolation of part of Damper (2-FCO-30-108) and Train B Gen Supply Fans 2A-A opens. in refueling area signal ductwork on Unit 2 2-FCO-30-109 (2-FCO-30-109) dampers, in and 2B-B and to failure; HS failure to side of AB. provides series, are provided with establish boundary for spring return from isolation and non-safety control air and both ABGTS. open to A-Auto. maintains the dampers fail closed on loss of ABSCE. control air. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE Instrumentation Requirements mitigation.
WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 12 of 27)
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 20 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 2-FCO-30-109 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate AB or spuriously Train B ABI or high rad isolation of part of Damper (2-FCO-30-108) and Train B Gen Supply Fans 2A-A opens. in refueling area signal ductwork on Unit 2 2-FCO-30-108 (2-FCO-30-109) dampers, in and 2B-B and to failure; HS failure to side of AB. provides series, are provided with establish boundary for spring return from isolation and non-safety control air and both ABGTS. open to A-Auto. maintains the dampers fail closed on loss of ABSCE. control air. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
21 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1-FCO-30-160 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate AB or spuriously Train A ABI or high rad isolation of AB Gen Damper (1-FCO-30-160) and Train B Gen Exhaust Fan 1A-A opens. in refueling area signal Exhaust Fan 1A-A. 1-FCO-30-161 (1-FCO-30-161) dampers, in suction and to establish failure; HS failure to provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air. Loss of the open to A-Auto. maintains the non-safety related control air does ABSCE. not prevent the damper from closing. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
6.2.3-55 WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 13 of 27) 6.2.3-56 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 22 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1-FCO-30-161 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train B Train B signal to isolate AB or spuriously Train B ABI or high rad isolation of AB Gen Damper (1-FCO-30-160) and Train B Gen Exhaust Fan 1A-A opens. in refueling area signal Exhaust Fan 1A-A. 1-FCO-30-160 (1-FCO-30-161) dampers, in suction and to establish failure; HS failure to provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air. Loss of the open to A-Auto. maintains the non-safety related control air does ABSCE. not prevent the damper from closing. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
23 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1-FCO-30-166 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate AB or spuriously Train A ABI or high rad isolation of AB Gen Damper (1-FCO-30-166) and Train B Gen Exhaust Fan 1B-B opens. in refueling area signal Exhaust Fan 1B-B. 1-FCO-30-167 (1-FCO-30-167) dampers, in suction and to establish failure; HS failure to provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air. Loss of the open to A-Auto. maintains the non-safety related control air does ABSCE. not prevent the damper from closing. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed Instrumentation Requirements since the damper has no safety function to open for DBE mitigation.
WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 14 of 27)
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 24 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1-FCO-30-167 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate AB or spuriously Train B ABI or high rad isolation of AB Gen Damper (1-FCO-30-166) and Train B Gen Exhaust Fan 1B-B opens. in refueling area signal Exhaust Fan 1B-B. 1-FCO-30-166 (1-FCO-30-167) dampers, in suction and to establish failure; HS failure to provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air. Loss of the open to A-Auto. maintains the non-safety related control air does ABSCE. not prevent the damper from closing. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
25 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 2-FCO-30-271 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate AB or spuriously Train A ABI or high rad isolation of AB Gen Damper (2-FCO-30-271) and Train B Gen Exhaust Fan 2A-A opens. in refueling area signal Exhaust Fan 2A-A. 2-FCO-30-272 (2-FCO-30-272) dampers, in suction and to establish failure; HS failure to provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air. Loss of the open to A-Auto. maintains the non-safety related control air does ABSCE. not prevent the damper from closing. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
6.2.3-57 WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 15 of 27) 6.2.3-58 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 26 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 2-FCO-30-272 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate AB or spuriously Train B ABI or high rad isolation of AB Gen Damper (2-FCO-30-271) and Train B Gen Exhaust Fan 2A-A opens. in refueling area signal Exhaust Fan 2A-A. 2-FCO-30-271 (2-FCO-30-272) dampers, in suction and to establish failure; HS failure to provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air. Loss of the open to A-Auto. maintains the non-safety related control air does ABSCE. not prevent the damper from closing. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
27 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 2-FCO-30-275 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate AB or spuriously Train A ABI or high rad isolation of AB Gen Damper (2-FCV-30-275) and Train B Gen Exhaust Fan 2B-B opens. in refueling area signal Exhaust Fan 2B-B. 2-FCO-30-276 (2-FCV-30-276) dampers, in suction and Exhaust failure; HS failure to provides series, are provided with Fan B-B and to spring return from isolation and non-safety control air. Loss of the establish boundary for open to A-Auto. maintains the non-safety related control air does ABGTS. ABSCE. not prevent the damper from closing. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed Instrumentation Requirements since the damper has no safety function to open for DBE mitigation.
WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 16 of 27)
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 28 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 2-FCO-30-276 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate AB or spuriously Train B ABI or high rad isolation of AB Gen Damper (2-FCV-30-275) and Train B Gen Exhaust Fan 2B-B opens. in refueling area signal Exhaust Fan 2B-B. 2-FCO-30-275 (2-FCV-30-276) dampers, in suction area and to failure; HS failure to provides series, are provided with establish boundary for spring return from isolation and non-safety control air. Loss of the ABGTS. open to A-Auto. maintains the non-safety related control air does ABSCE. not prevent the damper from closing. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
29 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1,2-FCO-30-294 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A** signal to isolate Purge or spuriously Train A ABI or high rad isolation of Purge Damper 1,2- (1,2-FCV-30-294) and Train B Air Supply Fan inlet opens. in refueling area signal Air Supply Fan inlet FCO-30-295 (1,2-FCV-30-295) dampers, in duct and to establish failure; HS failure to duct. provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air and both open to A-Auto. maintains the dampers fail closed on loss of ABSCE. control air. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Solenoid circuits for 1,2-FCO-30-294 and 1,2-FCO-30-295 are independent, with trained Class 1E power and trained ABI signal.
Damper failure to open is not listed since the damper has no safety function to open for DBE WBNP-112 mitigation.
6.2.3-59
- Unit 2 component, 2-FCO-30-294, was added for dual unit operation.
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 17 of 27) 6.2.3-60 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 30 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1,2-FCO-30-295 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B** signal to isolate Purge or spuriously Train B ABI or high rad isolation of Purge Damper 1,2- (1,2-FCV-30-294) and Train B Air Supply Fan inlet opens. in refueling area signal Air Supply Fan inlet FCO-30-294 (1,2-FCV-30-295) dampers, in duct and to establish failure; HS failure to duct. provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air and both open to A-Auto. maintains the dampers fail closed on loss of ABSCE. control air. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Solenoid circuits for 1,2-FCO-30-294 and 1,2-FCO-30-295 are independent, with trained Class 1E power and trained ABI signal.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
31 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-30-122 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate the or spuriously Train A ABI or high rad isolation of cask Damper (0-FCO-30-122) and Train B cask loading area opens. in refueling area signal loading area 0-FCO-30-123 (0-FCO-30-123) dampers, in exhaust and to failure; HS failure to exhaust. provides series, are provided with establish boundary for spring return from isolation and non-safety control air and both ABGTS. open to A-Auto. maintains the dampers fail closed on loss of Damper re-opens on ABSCE. control air. Independence of Instrumentation Requirements loss (or RESET) of ABI Train A and Train B isolation signal. signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE WBNP-112 mitigation.
- Unit 2 component, 2-FCO-30-294, was added for dual unit operation.
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 18 of 27)
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 32 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-30-123 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate the or spuriously Train B ABI or high rad isolation of cask Damper (0-FCO-30-122) and Train B cask loading area opens. in refueling area signal loading area 0-FCO-30-122 (0-FCO-30-123) dampers, in exhaust and to failure; HS failure to exhaust. provides series, are provided with establish boundary for spring return from isolation and non-safety control air and both ABGTS. open to A-Auto. maintains the dampers fail closed on loss of Damper re-opens on ABSCE. control air. Independence of loss (or RESET) of ABI Train A and Train B isolation signal. signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
33 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Train B Damper fails closed on loss of 0-FCO-30-129 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Damper 0- Train A 125 Vdc power. Train A Train A signal to isolate the or spuriously Train A ABI or high rad isolation of cask FCO-30-130 (0-FCO-30-129) and Train B cask loading area opens. in refueling area signal loading area provides (0-FCO-30-130) dampers, in supply and to establish failure; HS failure to supply. isolation and series, are provided with boundary for ABGTS. spring return from maintains the non-safety control air and both open to A-Auto. ABSCE. dampers fail closed on loss of control air. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
6.2.3-61 WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 19 of 27) 6.2.3-62 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 34 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-30-130 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate the or spuriously Train B ABI or high rad isolation of cask Damper (0-FCO-30-129) and Train B cask loading area opens. in refueling area signal loading area 0-FCO-30-129 (0-FCO-30-130) dampers, in supply and to establish failure; HS failure to supply. provides series, are provided with boundary for ABGTS. spring return from isolation and non-safety control air and both open to A-Auto. maintains the dampers fail closed on loss of ABSCE. control air. Independence of Train A and Train B isolation signals is discussed in "Remarks" under Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
35 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-31-350 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate PASF or spuriously Train A ABI or high rad isolation of PASF Damper (0-FCO-31-350) and Train B outside air intake and to opens. in refueling area signal outside air intake. 0-FCO-31-365 (0-FCO-31-365) dampers are in establish boundary for failure; HS failure to provides series. Independence of Train A ABGTS. spring return from isolation and and Train B isolation signals is open to A-Auto. maintains the discussed in "Remarks" under ABSCE. Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
Instrumentation Requirements WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 20 of 27)
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 36 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 0-FCO-31-365 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate PASF or spuriously Train B ABI or high rad isolation of PASF Damper (0-FCV-31-350) and Train B outside air intake and to opens. in refueling area signal outside air intake. 0-FCO-31-350 (0-FCV-31-365) dampers are in establish boundary for failure; HS failure to provides series. Independence of Train A ABGTS. spring return from isolation and and Train B isolation signals is open to A-Auto. maintains the discussed in "Remarks" under ABSCE. Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
37 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1,2-FCO-31-342 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train B Train A 125 Vdc power. Train A Train A signal to isolate PASF or spuriously Train A ABI or high rad isolation of PASF Damper 1,2- (1,2-FCO-31-342) and Train B Room No. 1 exhaust opens. in refueling area signal Room No. 1 FCO-31-343 (1,2-FCO-31-343) dampers are in and to establish failure; HS failure to exhaust. provides series. Independence of Train A boundary for ABGTS. spring return from isolation and and Train B isolation signals is open to A-Auto. maintains the discussed in "Remarks" under ABSCE. Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety function to open for DBE mitigation.
38 Isolation Damper Closes on ABI or high Stuck open, Mechanical failure; hot Indicating light in Loss of None. Damper fails closed on loss of 1,2-FCO-31-343 rad in refueling area fails to close, short in control wiring; the MCR. redundancy in Train A Train B 125 Vdc power. Train A Train B signal to isolate PASF or spuriously Train B ABI or high rad isolation of PASF Damper 1,2- (1,2-FCO-31-342) and Train B Room No. 1 exhaust opens. in refueling area signal Room No. 1 FCO-31-342 (1,2-FCO-31-343) dampers are in and to establish failure; HS failure to exhaust. provides series. Independence of Train A boundary for ABGTS. spring return from isolation and and Train B isolation signals is open to A-Auto. maintains the discussed in "Remarks" under ABSCE. Items 1 and 2 of this table.
Damper failure to open is not listed since the damper has no safety WBNP-112 function to open for DBE 6.2.3-63 mitigation.
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 21 of 27) 6.2.3-64 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 39 Modulating Regulates the amount Allows more Train A vital ac power "Hi Press. in Aux. See "Remarks" None. See ABI signal stops AB gen supply Damper of outside air to outside air failure; Train A aux. Bldg." alarm. column. "Remarks" fans automatically. The Aux. Bldg.
0-FCO-30-149 maintain ABSCE at than required control air failure; column. is designed for minimum leakage Train A -0.25 in w.g. (stuck open or spurious high dP and, with at least one ABGTS spuriously signal; failure of E/I or exhaust fan running, failure of the excessive) I/P converter; modulating damper can cause positioner mechanical pressure in the Aux. Bldg. to failure. approach outside pressure, but the AB pressure cannot become positive with respect to the outside.
The DPIS used for alarm in the control room is separate and independent from the DPIS used for modulating control of the damper. If the (non-safety) alarm functions, the operator can either close the associated Isolation Damper 0-FCO-30-280 or, if only one ABGTS exhaust fan is in operation, can start the redundant fan to maintain the -0.25 in w.g.
pressure.
Does not allow Train A vital ac power None. None (See Modulating Dampers the required failure; Train A aux. Train B Modulating note on items 0-FCO-30-148 and amount of control air failure; Damper 3 and 4.) 0-FCO-30-149 are provided with outside air spurious dP signal; 0-FCO-30-148 will train-separated, safety-grade (Stuck closed from 0-FCO-30-149; open to allow auxiliary control air.
or spurious failure of E/I or I/P sufficient outside inadequate converter; positioner air to control the opening). mechanical failure. negative pressure.
Instrumentation Requirements WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 22 of 27)
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 40 Modulating Regulates the amount Allows more Train B vital ac power "Hi Press. in Aux. See "Remarks" None. See ABI signal stops AB gen supply Damper of outside air to outside air failure; Train B aux. Bldg." alarm. column. "Remarks" fans automatically. The Aux. Bldg.
0-FCO-30-148 maintain ABSCE at than required control air failure; column. is designed for minimum leakage Train B -0.25 in w.g. (stuck open or spurious high dP and, with no air coming in and with spuriously signal; failure of E/I or at least one ABGTS exhaust fan excessive I/P converter; running, failure of the modulating opening). positioner mechanical damper can result in pressure in failure. the Aux. Bldg. approaching outside pressure, but the AB pressure cannot become positive with respect to the outside. The DPIS used for alarm in the control room is separate and independent from the DPIS used for modulating control of the damper. If the (non-safety) alarm functions, operator can either close the associated Isolation Damper 0-FCO-30-280 or, if only one ABGTS exhaust fan is in operation, can start the redundant fan to maintain -0.25 in w.g.
Does not allow Train B vital ac power None. None (See Modulating Dampers the required failure; Train B aux. Train A Modulating note on items 0-FCO-30-148 and amount of control air failure; Damper 3 and 4.) 0-FCO-30-149 are provided with outside air spurious dP signal; 0-FCO-30-149 will train-separated, safety-grade (Stuck closed from 0-FCO-30-149; open to allow auxiliary control air.
or spurious failure of E/I or I/P sufficient outside inadequate converter; positioner air to control the opening). mechanical failure. negative pressure.
6.2.3-65 WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 23 of 27) 6.2.3-66 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 41 ABGTS Vacuum Provides flow path for Fails to open, Mechanical failure; Indicating light in Aux. Bldg. at more None. See Dampers 0-FCO-30-279 and Relief Line outside air. stuck closed, Train A power failure; the MCR. negative pressure "Remarks" 0-FCO-30-280 are provided with Isolation Damper or spuriously Train A aux. control air (lower absolute column. train-separated, safety-grade 0-FCO-30-280 closes. failure; operator error pressure) than auxiliary control air. In addition, Train A (HS in wrong position). required to prevent there are two vacuum breaker leakage from dampers, 0-DMP-30-1128 and 0-outside. DMP-30-1129 in series which will admit outside air into the Bldg in case of increasing vacuum (more negative pressure).
Fails to close, Mechanical failure; Indicating light in None. Modulating None. The modulating damper cannot stuck open, or operator error (HS in the MCR. Damper shut off outside air completely.
spuriously wrong position). 0-FCO-30-149 can However, the amount of air passed opens. independently will be insignificant to cause control amount of pressure control problem.
outside air.
42 ABGTS Vacuum Provides flow path for Fails to open, Mechanical failure; Indicating light in Aux. Bldg. at more None. See Dampers 0-FCO-30-279 and Relief Line outside air. stuck closed, Train B power failure; the MCR. negative pressure "Remarks" 0-FCO-30-280 are provided with Isolation Damper or spuriously Train B aux. control air (lower absolute column. train-separated, safety-grade 0-FCO-30-279 closes. failure; operator error pressure) than auxiliary control air. In addition, Train B (HS in wrong position). required to prevent there are two vacuum breaker leakage from dampers, 0-DMP-30-1128 and 0-outside. DMP-30-1129 in series which will admit outside air into the Bldg in case of increasing vacuum.
Fails to close, Mechanical failure; Indicating light in None. Modulating None The modulating damper cannot stuck open, or operator error (HS in the MCR. Damper shut off outside air completely.
spuriously wrong position). 0-FCO-30-148 can However, the amount of air passed Instrumentation Requirements opens. independently will be insignificant to cause control amount of pressure control problem.
outside air.
WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 24 of 27)
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 43 Train A Provides Class 1E Loss of or Diesel generator Alarm and Loss of None. Train A isolation dampers are not Emergency diesel-backed power inadequate failure; bus fault indication in the redundancy in Redundant directly affected since damper Power supply to active voltage. (Train A); operator MCR. ABGTS exhaust Train B solenoids and control circuits are components of Train A error. flow paths. exhaust fan supplied either battery power or of ABGTS. can maintain battery-backed vital ac power.
required Loss of power to the damper negative control circuits does not result in pressure. loss of redundancy since circuits are such that isolation dampers fail closed.
44 Train B Provides Class 1E Loss of or Diesel generator Alarm and Loss of None. Train B isolation dampers are not Emergency diesel-backed power inadequate failure; bus fault indication in the redundancy in Redundant directly affected since damper Power supply to active voltage. (Train B); operator MCR. ABGTS exhaust Train A solenoids and control circuits are components of Train B error. flow paths. exhaust fan supplied either battery power or of ABGTS. can maintain battery-backed vital ac power.
required Loss of power to the damper negative control circuits does not result in pressure. loss of redundancy since circuits are such that isolation dampers fail closed.
45 Aux. Bldg. Provides flow path for Fails to open; Mechanical Failure Visual Aux. Bldg at more None. This damper will only be used in vacuum relief outside air. stuck closed. negative pressure the event that isolation dampers damper (lower absolute 0-DMP-30-279 and 0-DMP-30-280 0-DMP-30-1128 pressure) than fail close. Therefore, for this required to prevent damper to fail close, and one of the leakage to outside. isolation dampers to fail close at the same time would constitute a double failure.
Fails to close, Mechanical Failure Visual None. Vacuum relief dampers stuck open. Vacuum relief 0-DMP-30-1128 and damper 0-DMP-30-1129 are installed in 0-DMP-30-1129 series.
can close independently and WBNP-112 eliminate flow path from outside air.
6.2.3-67
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 25 of 27) 6.2.3-68 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 46 Aux. Bldg. Provides flow path for Fails to open; Mechanical Failure Visual Aux. Bldg. at more None. This damper will only be used in vacuum relief outside air. stuck closed. negative pressure the event that isolation damper damper (lower absolute 0-DMP-30-279 and 0-DMP-30-280 0-DMP-30-1129 pressure) than fail close. Therefore, for this required to prevent damper to fail close, and one of the leakage to outside. isolation dampers to fail close at the same time would constitute a double failure.
Fails to close; Mechanical Failure Visual None. Vacuum None (See Vacuum relief damper stuck open. relief damper Remarks) 0-DMP-30-1128 and 0-DMP-30-1128 0-DMP-30-1129 are installed in can close series.
independently and eliminate flow path from outside air.
Instrumentation Requirements WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 26 of 27)
Instrumentation Requirements WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 47 Fire Dampers Provide air flow path for Spurious Failure of fusible link. Low flow alarm. Loss of Train B None (See Fire dampers are safety-related; 0-ISV-31-3834 common duct between closure. Remarks). their failure constitutes a single and ABGTS fans. failure. Therefore, both ABGTS 0-ISV-31-3845 trains would be available.
48 Deluge System Floods the carbon Spurious Failure of fusible link. ----- None (See None (See Opposite train ACU is independent (Spray heads adsorbers in event of opening of Remarks) Remarks). and remains available, or deluge and piping inside fire. spray heads, Loss of piping valve remains closed in the ACU A-A or B-B) or piping pressure boundary. absence of heat detection.
failure 48b Deluge Valve Discharge water in Spurious - Mechanical failure Local and MCR None (See None (See ACU will not be flooded since the 1-FCV-26-163 event of fire in carbon actuation or alarms on water Remarks) Remarks) fusible links on the spray heads will adsorbers. - Electrical failure discharge be intact due to absence of heat.
48c Deluge Valve Discharge water in Spurious - Mechanical failure Local and MCR None (See None (See ACU will not be flooded since the 2-FCV-26-171 event of fire in carbon actuation or alarms on water Remarks) Remarks) fusible links on the spray heads will adsorbers. - Electrical failure discharge be intact due to absence of heat.
49 Ductwork in the Provides containment Leakage. Cracks. ---- Minimal localized None (See Only small cracks are postulated ABSCE for air flow path. reduction of Remarks) due to seismic qualification.
negative pressure. Minimal localized reduction of negative pressure will not affect the ABSCE.
Loss of fluid (air) is not a concern since the system is submerged in the same fluid.
6.2.3-69 WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis For Passive Failure for the ABGTS (Page 27 of 27) 6.2.3-70 WATTS BAR ITEM FAILURE METHOD OF EFFECT ON EFFECT ON NO. COMPONENT FUNCTION MODE POTENTIAL CAUSE DETECTION SYSTEM PLANT REMARKS 50 ABGTS Air Controls humidity of Fails to turn on Train A power failure; Hi Rad alarm in the Loss of None (See 1. Failure to cutout is not Cleanup Unit A exhaust air. or fails to temperature sensing MCR for air to redundancy in Remarks) considered in this table since Heater operate. error. Shield Bldg. vent. ABGTS. Failure of this is the safe position for heater will allow controlling air humidity.
humid air into carbon filter 2. The air temperature for the reducing its switch, 0-TS-30-143, for this efficiency (see heater is sensed by a "Remark #3"). non-safety related sensor, 0-TE-30-143. DCN M-21750 has been initiated to resolve this problem. Section 8.2 address this further.
- 3. Heater operation is tested every 31 days per procedure.
51 ABGTS Air Controls humidity of Fails to turn on Train B power failure; Hi Rad alarm in the Loss of None (See 1. Failure to cutout is not Cleanup Unit B exhaust air. or fails to temperature sensing MCR for air to redundancy in Remarks) considered in this table since Heater operate. error. Shield Bldg. vent. ABGTS. Failure of this is the safe position for heater will allow controlling air humidity.
humid air into carbon filter 2. The air temperature for the reducing its switch, 0-TS-30-143, for this efficiency (see heater is sensed by a "Remark #3"). non-safety related sensor, 0-TE-30-143. DCN M-2175 has been initiated to resolve this problem. Section 8.2 address this further.
- 3. Heater operation is tested every Instrumentation Requirements 31 days per procedure.
WBNP-112
Instrumentation Requirements WATTS BAR Table 6.2.3-3 Failure Modes and Effects Analysis for the ABGTS NOTES FOR ABGTS FAN FAILURE MODES AND THEIR IMPACT ON THE EGTS POST-ACCIDENT TIME INTERVAL EGTS ABGTS REMARKS 0 - 30 minutes 2 fans (auto start) 2 fans (auto start) 2 EGTS fans together produced -2.3 w.g. dP in the annulus more than the dP of
-0.69 w.g. effected by the ABGTS fans in ABSCE.
1 fan operating 2 fans (auto start) 2 ABGTS fans together pulled a vacuum of -0.69 w.g. @ Elevation 763.0 of the ABSCE, whereas, 1 EGTS fan drew down the annulus to -1.15 w.g., thus attesting 1 fan failed that the annulus dPs are more negative than ABSCE.
2 fans (auto start) 2 fans (auto start) 2 ABGTS fans together drew down the ABSCE to -1.09 w.g. @ Elevation 763.0 of the ABSCE, whereas, the 2 EGTS fan together produced -2.3 w.g. in the annulus.
Therefore, the annulus dP remains more negative.
1 fan operating 2 fans (auto start) The failure of two safety-related components (i.e., fan and a damper affecting the same parameter, namely the annulus dP, is not postulated. Therefore, this failure mode is invalid.
> 30 minutes 1 fan (operating) 1 fan (operating) 1 EGTS fan produces more negative dP in the annulus than 1 ABGTS fan in the ABSCE 1 fan (shutdown by operator) 1 fan (shutdown by operator) 1 fan (operating) 1 fan (operating) 2 ABGTS fans together produced a dP of -0.69 w.g. @ Elevation 763.0 of AB; whereas, 1 EGTS fan drew down the annulus to -1.15 w.g. @ Elevation 783.0.
Therefore, the annulus is more negative than ABSCE.
1 fan (operating) 2 fans (operator is yet to shutdown 2 ABGTS fans together drew down the ABSCE to -1.09 w.g. @ Elevation 763.0, one of the fans) whereas 1 EGTS fan was able to maintain -1.15 w.g. @ Elevation 783.0 of the annulus. However, in a later test, the same EGTS fan maintained -1.05 w.g.
1 fan (shutdown by operator) 1 vacuum relief damper failed However, the dP in the ABSCE remained less negative than that of the annulus.
6.2.3-71 WBNP-112
Table 6.2.3-3 Failure Modes and Effects Analysis for the ABGTS 6.2.3-72 WATTS BAR NOTES FOR ABGTS FAN FAILURE MODES AND THEIR IMPACT ON THE EGTS POST-ACCIDENT TIME INTERVAL EGTS ABGTS REMARKS 0 - 30 minutes 2 fans (auto start) 2 fans (auto start) 2 EGTS fans together produced -2.3 w.g. dP in the annulus more than the dP of -
0.69 w.g. effected by the ABGTS fans in ABSCE.
1 fan operating 2 fans (auto start) 2 ABGTS fans together pulled a vacuum of -0.69 w.g. @ Elevation 763.0 of the ABSCE, whereas, 1 EGTS fan drew down the annulus to -1.15 w.g., thus attesting 1 fan failed that the annulus dPs are more negative than ABSCE.
2 fans (auto start) 2 fans (auto start) 2 ABGTS fans together drew down the ABSCE to -1.09 w.g. @ Elevation 763.0 of the ABSCE, whereas, the 2 EGTS fan together produced -2.3 w.g. in the annulus.
Therefore, the annulus dP remains more negative.
1 fan operating 2 fans (auto start) The failure of two safety-related components (i.e., fan and a damper affecting the same parameter, namely the annulus dP, is not postulated). Therefore, this failure mode is invalid.
Instrumentation Requirements WBNP-112
WATTS BAR WBNP-112 Figure 6.2.3-1 Typical Mechanical Penetration Seals Secondary Containment Functional Design 6.2.3-73
WATTS BAR WBNP-112 Figure 6.2.3-2 Typical Purge Penetration Arrangement Secondary Containment Functional Design 6.2.3-74
WATTS BAR WBNP-112 Figure 6.2.3-3 Typical Electrical Penetrations Secondary Containment Functional Design 6.2.3-75
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-4 Auxiliary Building Isolation Barrier Secondary Containment Functional Design 6.2.3-76
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-5 Auxiliary Building Isolation Barrier Secondary Containment Functional Design 6.2.3-77
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-6 Auxiliary Building Isolation Barrier Secondary Containment Functional Design 6.2.3-78
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-7 Auxiliary Building Isolation Barrier Secondary Containment Functional Design 6.2.3-79
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-8 Auxiliary Building Isolation Barrier Secondary Containment Functional Design 6.2.3-80
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-9 Auxiliary Building Isolation Barrier Secondary Containment Functional Design 6.2.3-81
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-10 Auxiliary Building Isolation Barrier Secondary Containment Functional Design 6.2.3-82
WATTS BAR Secondary Containment Functional Design Figure 6.2.3-11 Reactor Building - Units 1 & 2 Flow Diagram - Heating and Ventilation Air Flow WBNP-112 6.2.3-83
WATTS BAR Secondary Containment Functional Design Figure 6.2.3-12 Powerhouse Units 1 & 2 Electrical Logic Diagram - Emergency Gas Treatment System WBNP-112 6.2.3-84
WATTS BAR Secondary Containment Functional Design Figure 6.2.3-13 Powerhouse Units 1 & 2 Electrical Logic Diagram - Emergency Gas Treatment WBNP-112 6.2.3-85
WATTS BAR Secondary Containment Functional Design Figure 6.2.3-14 Powerhouse Unit 1 Electrical Logic Diagram -Emergency Gas Treatment WBNP-112 6.2.3-86
WATTS BAR Secondary Containment Functional Design Figure 6.2.3-15 Powerhouse Units 1 & 2 Electrical Control Diagram - Emergency Gas Treatment System WBNP-112 6.2.3-87
WATTS BAR Secondary Containment Functional Design Figure 6.2.3-15-SH-A Powerhouse Unit 2 Electrical Control Diagram - Emergency Gas Treatment WBNP-112 6.2.3-88
WATTS BAR Secondary Containment Functional Design Figure 6.2.3-16 Powerhouse Units 1 & 2 Auxiliary Building -Flow Diagram -Heating & Ventilating Air Flow WBNP-112 6.2.3-89
WATTS BAR Secondary Containment Functional Design Figure 6.2.3-17A Post-Accident Annulus Pressure and Vent Flow Rate WBNP-112 6.2.3-90
WATTS BAR WBNP-112 Figure 6.2.3-17 Post-Accident Annulus Pressure and Reactor Unit Vent Flow Rate Transients Secondary Containment Functional Design 6.2.3-91
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-18 Reactor Building Units 1 & 2 Mechanical Heating and Ventilating Secondary Containment Functional Design 6.2.3-92
Security-Related Information - Withheld Under 10CFR2.390 WATTS BAR WBNP-112 Figure 6.2.3-19 Reactor Building Units 1 & 2 Mechanical Heating, Ventilation, And Air Conditioning Secondary Containment Functional Design 6.2.3-93
WATTS BAR WBNP-112 THIS PAGE INTENTIONALLY BLANK Secondary Containment Functional Design 6.2.3-94
WATTS BAR WBNP-112 6.2.4 Containment Isolation Systems The containment isolation systems provide the means of isolating fluid systems that pass through containment penetrations so as to confine to the containment any radioactivity that may be released in the containment following a design basis event.
The containment isolation systems are required to function following any design basis event that initiates a Phase A or Phase B containment isolation signal or releases radioactive materials into containment to isolate non-safety-related fluid systems penetrating the containment. The Watts Bar Nuclear Plant does not have a particular system for containment isolation, but isolation design is achieved by applying common criteria to penetrations in many different fluid systems and by using ESF signals to actuate appropriate valves.
6.2.4.1 Design Bases The main function of the containment isolation system is to provide containment integrity when needed. Containment integrity is defined to exist when:
(1) The non-automatic containment isolation valves and blind flanges are closed as required.
(2) The containment equipment hatch is properly closed.
(3) At least one door in each containment personnel air lock is properly closed.
(4) All automatic containment isolation valves are operable or are deactivated in the closed position or at least one valve in each line having an inoperable valve is closed.
(5) All requirements of the Technical Specification with regard to containment leakage and test frequency are satisfied.
Containment integrity is required if there is fuel in the reactor which has been used for power operation, except when the reactor is in the cold shutdown condition with the reactor vessel head installed, or when the reactor is in the refueling shutdown condition with the reactor vessel head removed. Containment isolation is not essential for design basis events, such as HELBs, outside containment which do not release radioactive materials into containment. The failure of containment isolation valves for such an event would not result in the release of radioactive fluids from inside containment.
In general, the containment isolation system is designed to the requirements of General Design Criteria 54, 55, 56, and 57 of 10 CFR 50, Appendix A. The following are alternate containment isolation provisions for certain classes of lines:
(1) Fluid instrument lines penetrating the containment are designed to meet the referenced General Design Criteria except for the pressure sensor and reactor vessel level instrumentation system lines. Instrument lines which penetrate containment are listed in Table 6.2.4-4.
Containment Isolation Systems 6.2.4-1
WATTS BAR WBNP-112 (2) Remote-manual valves are used for isolation provisions on certain lines associated with engineered safety features (such as the ECCS) instead of automatic isolation valves.
(3) A closed system outside the containment is acceptable as one of the two isolation barriers if designed to the following criteria:
(a) Does not communicate with the outside environment (b) Meets Safety Class 2 design requirements (c) Withstands the internal temperatures and pressures which occur as a result of the containment design basis events (d) Withstands loss-of-coolant accident transients and environment (e) Meets Seismic Category I design requirements (f) Protected against missiles, pipe whip, and jet impingement.
(4) The isolation function of an engineered safety feature or system required to test an engineered safety feature requires one barrier to remain functional after the occurrence of a single active failure. Normally, this is accomplished by providing two isolation valves in series. If it can be shown that a single active failure can be accommodated with only one valve in the line and that fluid system reliability is enhanced by having one valve rather than two valves in series, then one valve and a closed system both located outside of the containment are acceptable. The single valve and piping between the containment and the valve are enclosed in a protective leaktight housing to prevent leakage to the atmosphere in the event of external leakage.
(5) Relief valves may be used as isolation valves, provided the relief valve setpoint is greater than 1.5 times the containment design internal pressure.
The criteria for the number and location of containment isolation valves in each fluid system depend on the valves functions and whether they are open or closed to the containment atmosphere or reactor coolant system. Four isolation classes of fluid system penetrations are defined as follows:
(1) Isolation Class I - Fluid lines which are open to the atmosphere outside the containment and are connected to the reactor coolant system or are open to the containment atmosphere. Each isolation Class I system has a minimum of two isolation valves in series. Where system design permits, one valve is located inside and one valve is located outside containment.
(2) Isolation Class II - Fluid lines which are connected to a closed system outside the containment and are connected to the reactor coolant system or are open to the containment atmosphere. Also included in isolation Class II are fluid lines which are open to the atmosphere outside the containment and are 6.2.4-2 Containment Isolation Systems
WATTS BAR WBNP-112 separated from the reactor coolant system and the containment atmosphere by a closed system inside the containment. Each isolation Class II system has, as a minimum, one isolation valve.
(3) Isolation Class III - Fluid lines which are connected to a closed system both inside and outside the containment. Isolation Class III systems have, as a minimum, one isolation valve.
(4) Isolation Class IV - Fluid lines which must remain in service subsequent to a design basis event, such as lines serving ESF systems. Isolation valves on these lines are not automatically closed by the containment isolation signal.
Each isolation Class IV system has, as a minimum, one isolation valve (remote-manual operation).
The following design requirements for containment isolation barriers apply:
(1) The design pressure of all piping and connected equipment comprising the isolation boundary is equal to or greater than the design pressure of the containment.
(2) All valves and equipment which are considered to be isolation barriers and designed in accordance with Seismic Category I criteria shall be protected against missiles and jet impingement, both inside and outside the containment.
(3) All valves and equipment which are considered to be isolation barriers are designed, as a minimum, to ASME Section III Class 2 requirements except as noted in Item 1 of Section 6.2.4.2.1.
(4) A system is closed inside the containment if it meets all of the following:
(a) It does not communicate with either the reactor coolant system or the reactor containment atmosphere.
(b) It will withstand external pressure and temperature equal to containment structural integrity test pressure and design temperature.
(c) It will withstand accident temperature, pressure, and fluid velocity transients, and the resulting environment, including internal thermal expansion.
(d) It is protected against missiles, pipe whip, and jet impingement.
(5) A check valve inside the containment on the incoming line is considered an automatic isolation valve.
(6) A pressure relief valve that relieves toward the inside of the containment is considered an automatic isolation valve.
(7) A locked closed valve is considered an automatic isolation valve.
Containment Isolation Systems 6.2.4-3
WATTS BAR WBNP-112 (8) To qualify as an automatic isolation valve, an air-operated valve must fail closed on loss of air, power, etc.
(9) Valves used for containment isolation shall be designed capable of tight shutoff in order to limit gas leakage to a specific maximum amount at containment design pressure.
The design bases for the containment isolation system include provision for the following:
(1) A double barrier at the containment penetration in those fluid systems that are not required to function following a design basis event.
(2) Automatic, fast, efficient closure of those valves required to close for containment integrity following a design bases event to minimize release of any radioactive material.
(3) A means of leak testing barriers in fluid systems that serve as containment isolation.
(4) The capability to periodically test the operability of containment isolation valves.
6.2.4.2 System Design The containment isolation system meets the design bases presented in Section 6.2.4.1 with the exception of those cases which are discussed in detail in Section 6.2.4.3.
Containment isolation can be initiated by either Phase A or Phase B signals.
A Phase A signal is generated by either of the following:
(1) Manual - either of two momentary controls (2) A safety injection signal, generated by one or more of the following:
(a) Low steamline pressure in any steamline (b) Low pressurizer pressure (c) High containment pressure (d) Manual - either of two momentary controls.
6.2.4-4 Containment Isolation Systems
WATTS BAR WBNP-112 A Phase B signal is generated by either of the following:
(1) Manual - two sets (two switches per set) - actuation of both switches is necessary in either set for spray initiation (2) Automatic High-high containment pressure.
Containment isolation Phase A always exists if containment isolation Phase B exists, when the Phase B signal is initiated by automatic instrumentation. Phase A containment isolation does not occur when the Phase B signal is initiated manually.
The instrumentation circuits that generate both Phase A and Phase B signals are described in Chapter 7.
With the exception of the cases identified below, the containment isolation system provides for automatic, fast, and efficient closure of those valves required to close for containment integrity following a design basis event to minimize the release of any radioactive material. Closure times for isolation valves are included in Table 6.2.4-1.
With a single failure of containment isolation valves 1-FCV-32-110, 1-FCV-67-107, 1FCV-70-92 or 1-FCV-70-140, concurrent with an HELB inside containment such as a LOCA, Main Steam Line Break, or Feedwater Line Break, etc., manual actions are required to prevent the possibility of process fluid (air or water) from entering containment (See Tables 9.2-2, 9.2-9, and 9.3-7). Manual actions are required in these cases since a check valve serves as an inboard containment isolation valve, and pressure boundary integrity of the lines in containment past the check valves cannot be assured.
6.2.4.2.1 Design Requirements Containment isolation barrier design includes the following requirements:
(1) As a minimum, containment barriers are designed to ASME Section III Class 2 requirements. This design meets the requirements of Regulatory Guide 1.26 for the containment isolation systems, except that the four auxiliary feedwater lines incorporate safety-grade Quality Group C (ASME Section III, Class 3) valves outside containment for isolation. This has been documented in NUREG 0847 as acceptable to the NRC. Valves and equipment which are considered to be isolation barriers are designed to Seismic Category I requirements which is the intent of Regulatory Guide 1.29.
(2) Isolation barriers either inside or outside of the containment are protected against missiles, pipe whip, and jet impingement during a LOCA.
(3) Power operated isolation valves are tested for operability by the manufacturer and preoperationally after installation. Those automatic isolation valves with air or motor operators that do not restrict normal plant operation are periodically tested to ensure operability.
Additional design information is included in Table 6.2.4-1.
Containment Isolation Systems 6.2.4-5
WATTS BAR WBNP-112 6.2.4.2.2 Containment Isolation Operation A containment isolation signal initiates closing of automatic isolation valves in those lines which must be isolated immediately following a design basis event. The containment isolation valves will close within the time specified in Table 6.2.4-1.
However, on loss of ac power, the diesel will have to be started prior to closure. It is estimated that the time required to start the diesel is 10 seconds. The logic diagram for this system is shown in Figure 6.2.4-21.
Check valves are used under conditions where differential pressure will close the valves to maintain containment integrity. Lines which, for safety reasons, must remain in service subsequent to a design basis event are provided with at least one isolation valve.
Each automatic isolation valve required to operate subsequent to an accident is additionally provided with a manual control switch for operation. The position of these automatic isolation valves is indicated by status lights in the main control room.
Primary and secondary modes of valve actuation are shown in Table 6.2.4-1.
Redundant isolation barriers are used to prevent any single failure from causing an open path from the containment. If two power operated valves are used in series in a line for isolation purposes, one valve is supplied with one train of control and power and the other valve is supplied by the other train. Redundancy in power, signals, and barriers is provided to assume isolation.
Provisions for detecting leakage from remote manually controlled systems (such as the ECCS) include the use of pressure and flow meters, and inspection of the systems during normal plant operation. Details for leak detection are given in the appropriate system descriptions. Piping systems penetrating the containment have been provided with test vents and test connections or have other provisions to allow periodic leak testing (see Section 6.2.6). Test connections, vents and drains located within the containment boundary (between containment isolation valves) of penetrations subject to 10CFR50, Appendix J, Type C testing also have the capability of being leak tested or are one inch in size or less, administratively secured closed and consist of a double barrier (e.g. two valves in series, one valve with nipple and cap, one valve and a blind flange).
The manufacturers of isolation system components perform tests to demonstrate the ability of mechanical and electrical components located inside the containment to perform as required in the containment environment following the design basis accident. Accident conditions which are considered in the design of isolation components are pressure, humidity, radiation, and temperature. Section 3.11 gives information concerning the environmental conditions used in the design of the containment isolation system including more detail on qualification testing of ESF components.
The description and design requirements for the instrumentation and control portions of the containment isolation system are discussed in Chapter 7.
6.2.4-6 Containment Isolation Systems
WATTS BAR WBNP-112 6.2.4.2.3 Penetration Design The penetrations are classified into 24 different types. These are shown in Figures 6.2.4-1 through 6.2.4-17E.
The locations of these penetrations through the steel containment and the Shield Building are shown in Figures 6.2.4-18 and 6.2.4-19, respectively. The penetrations are tabulated in Table 6.2.4-1. The different types of penetrations are discussed below and the various possible leakage paths, as tabulated in Table 6.2.4-1 and shown in Figure 6.2.4-20, are also described below.
Penetration Types I and II - Main Steam and Feedwater The main steam and feedwater line penetrations, shown in Figures 6.2.4-1 and 6.2.4-2, are the "hot" type in which the penetrations must accommodate thermal movement. Each "hot" process line where it passes through the containment penetration is enclosed in a guard pipe that is attached to the process line through a multiple fluid fitting. The guard pipe protects the bellows should the process line fail within the annulus between the containment vessel and the Shield Building, thereby precluding the discharge of fluids into the annulus. The inner end of the guard pipe is fitted with an impingement ring which protects the bellows from jets originating from pipe breaks inside containment. In addition, the guard pipe for this type of penetration extends through and is supported by the crane wall. This avoids transmitting loads to the containment vessel. Also, in the event of a pipe rupture it discharges fluid into the reactor compartment rather than smaller rooms outside the crane wall, thus preventing, overpressurization of these smaller rooms.
For each of these penetrations the penetration sleeve is welded to the containment vessel. The process line which passes through the penetration is allowed to move both axially and laterally. A two-ply bellows expansion joint is provided to accommodate any movement between the containment vessel and the Shield Building, under any conditions. The bellows is designed to withstand containment design pressure. When an embedded anchor is not utilized, a low-pressure flexible closure will seal the process line to the sleeve in the Shield Building, which will not impose significant stress on the penetration.
The flexible closure described above is located outdoors and serves to contain leakage from the flued head so that the leakage is routed back to the annulus, and to seal the annulus from the outdoors.
Guides and anchors limit movement of pipes such that design limits on the containment penetration and bellows are not exceeded during conditions of plant operation, test, or postulated accidents.
Penetration Type III - Residual Heat Removal Pump Supply and Return The RHR pump supply and return penetrations, shown in Figure 6.2.4-3, are also the "hot" type. For these penetrations, the guard pipe does not penetrate the crane wall.
This type of penetration is anchored at the Shield Building wall in addition to being Containment Isolation Systems 6.2.4-7
WATTS BAR WBNP-112 supported from the internal concrete structure to minimize loads transmitted to the steel containment vessel.
The Shield Building sleeves have embedded anchors and the flued heads are in the Auxiliary Building. There is no need for low-pressure flexible closures as used in penetrations types I and II, since any leakage from the flued head will be processed by the auxiliary building gas treatment system.
Penetration Types IV and V Types IV and V penetrations are also thermally "hot" with insulation and bellows, as shown in Figure 6.2.4-4. Any leakage through the flued heads or through the bellow will be into the annulus and thereby processed by the emergency gas treatment system. The two types differ by only the weld ends.
Penetration Types VI, VII, and VIII Penetrations types VI through X and XIII through XVIII are "cold" penetrations.
For "cold" piping penetrations, a low-pressure flexible closure will seal the cold pipe to the sleeve penetrating the Shield Building. The piping configuration and supports on either side of the penetration will be designed to preclude overstressing the containment vessel at the penetration under any conditions, including postulated accidents.
Relatively small thermal movement or stress is expected for the "cold" penetrations.
The clearance space provided for the pipe going through the Shield Building wall is computed by the summation of the relative movements of the pipe and the Shield Building . Ample clearance space is provided so that the pipe will not be in contact with the Shield Building sleeve under any condition.
Penetration types VI and VII have provisions for dissimilar metal welding. The two types differ in their weld ends only. Penetration types VI and VII are illustrated in Figure 6.2.4-5. The flued heads of both types are located in the annulus.
Penetration type VIII is similar to that of penetrations types VI and VII, except that there is no dissimilar metal weld. Penetration type VIII is illustrated in Figure 6.2.4-6.
Penetration Type IX Containment Spray and RHR Spray Headers There is no difference between penetration types VII and IX except that penetration type IX is located at the dome. Penetration type IX is illustrated in Figure 6.2.4-7. The flued heads are located in the annulus.
Penetration Type X - Multiple Line Sleeves Type X penetrations are primarily for instrumentation lines such as sampling and monitor lines. Typical multiple line sleeves are shown in Figure 6.2.4-8.
6.2.4-8 Containment Isolation Systems
WATTS BAR WBNP-112 Penetration Types XI and XII - Emergency Sump During long-term post-accident conditions, containment sump water is recirculated through the RHR system and the containment spray system. The water collects on the floor of the containment and flows to the emergency sump. The water flows out of the containment through two type XII penetrations shown in Figure 6.2.4-9. Each line contains an isolation valve enclosed in a valve compartment. The valve compartments are designed for the same conditions as the containment except for leaktightness. The penetration between each valve compartment and the Auxiliary Building is a type XI penetration illustrated in Figure 6.2.4-10.
The type XII penetration has a flued head located in the containment sump. The outer sleeve (guard pipe) of the flued head is welded directly to the containment liner which is completely embedded in the concrete.
The type XI penetration has the flued head located in the Auxiliary Building. The penetration is insulated because of the hot sump water which would pass through it in the event of a design bases event.
Penetration Type XIII - Ventilation Heating and ventilation ducts utilize penetration type XIII, as shown in Figure 6.2.4-11.
Process lines are welded directly to these penetrations. Additional information on ventilation duct penetrations is given in Section 6.2.4.3.1 on possible leakage paths.
Penetration Type XIV - Equipment Hatch An equipment hatch fabricated from welded steel and furnished with a double-gasketed flange and bolted dished door is provided. A test connection to the space between the gaskets is provided to pressurize the space for leak rate testing, as shown in Figure 6.2.4-12.
Penetration Type XV - Personnel Access Two personnel air locks are provided. Each personnel air lock, as shown in Figure 6.2.4-13, is a double door welded steel assembly. Quick-acting type equalizing valves are provided to equalize pressure in the air lock when personnel enter or leave the containment vessel. The doors are sealed with double gaskets. A test connection to the space between the gaskets is provided to pressurize the space for leak rate testing.
The emergency air supply connection to the space between the double doors serves as a test connection to pressurize this space for leak rate testing. A special hold-down device is provided to secure the inner door in a sealed position during leak rate testing of the space between the doors.
The two doors in each personnel air lock are interlocked to prevent both being opened simultaneously and to ensure that one door and its equalizing valve are completely closed before the opposite door can be opened. Remote indicating lights and annunciators located in the main control room indicate the door is in operational status.
Provision is made to permit bypassing the door interlocking system with a special tool to allow doors to be left, open during plant cold shutdown. Both doors may also be left Containment Isolation Systems 6.2.4-9
WATTS BAR WBNP-112 open during fuel handling activities under special administrative controls as discussed in Section 6.2.3.2.1. Each lock door hinge is designed to be capable of adjustment to assure proper seating. A lighting and communication system is provided in the lock interior.
Penetration Type XVI - Fuel Transfer Tube A 20-inch OD fuel transfer tube penetration is provided for fuel movement between the refueling canal in the containment and the spent fuel pool. The penetration consists of 20-in stainless steel pipe installed inside a 24-inch carbon steel pipe, as shown on Figure 6.2.4-14. The inner pipe acts as the transfer tube and is fitted with a double gasketed blind flange in the refueling canal and a standard gate valve in the spent fuel pool. The inner pipe is welded to the containment penetration sleeve. Bellows expansion joints are provided on the pipes to compensate for any differential movement between the two pipes or other structures.
Penetration Type XVII - Incore Instrumentation Thimble Assembly (IITA)
Renewal Incore instrumentation thimble assembly (IITA) renewal requires penetrations in both the steel containment and the Shield Building at the same elevation and azimuth.
These are separate penetrations and are not connected in the annulus. The containment penetration, illustrated in Figure 6.2.4-15, has a blind flange with double O-rings and a leak rate test connector installed inside the annulus. The shield building penetration utilizes a raised face blind flange with a single gasket installed outside the shield building.
Penetration Type - XVIII - Ice Blowing The ice blowing line penetration has a blind flange with double O-rings installed on the outside of the containment as shown in Figure 6.2.4-16. Sealing between the outside and the annulus penetration through the shield wall is provided by a blind flange fitted with a gasket installed on the inside and outside of the Shield Building penetration.
Penetration Type XIX - Electrical The electrical penetration assemblies provide a means for the continuity of power, control, and signal circuits through the primary containment structure.
Each assembly consists of redundant pressure barriers through which the electrical conductors are passed, as shown in Figure 6.2.4-17.
Each penetration assembly is sized such that it may be inserted into and be compatible with the penetration nozzles which are furnished as a part of the containment structure.
Unless otherwise specified, the assembly is designed to be inserted from the outboard-end of the primary containment nozzle.
The criteria and requirements for the design, construction, and installation of the modular type electrical penetrations conform to IEEE Standard 317-1976, "IEEE 6.2.4-10 Containment Isolation Systems
WATTS BAR WBNP-112 Standard for Electrical Penetration Assemblies in Containment Structures for Nuclear Fueled Power Generating Stations."
The criteria and requirements for the design construction and installation of fiber optic feed-throughs in modular type electrical penetrations conform to IEEE Standard 317-1983. IEEE Standard for Electric Penetration Assemblies in Containment Structures for Nuclear Power Generating Station.
Penetration Type XX The feedwater bypass line penetrations, shown in Figure 6.2.4-17A are the 'hot' type in which the penetrations must accommodate thermal movement. Each 'hot' process line where it passes through the containment penetration is enclosed in a guard pipe that is attached to the process line through a multiple fluid fitting. The guard pipe protects the bellows should the process line fail within the annulus between the containment vessel, thereby precluding the discharge of fluids into the annulus. The inner end of the guard pipe is fitted with an impingement ring which protects the bellows from jets originating from pipe breaks inside containment. In addition, the guard-pipe for this type of penetration extends through and is supported by the crane wall. This avoids transmitting loads to the containment vessel. Also, in the event of a pipe rupture it discharges fluid into the reactor compartment rather than smaller rooms outside the crane wall, thus preventing overpressurization of these smaller rooms.
For each of these penetrations, the penetration sleeve is welded to the containment vessel. The process line which passes through the penetration is allowed to move both axially and laterally. A two-ply bellows expansion joint is provided to accommodate movement between the containment vessel and the Shield Building. The bellows is designed to withstand containment design pressure. When an embedded anchor is not utilized, a low-pressure flexible closure will seal the process line to the sleeve in the Shield Building, which will not impose significant stress on the penetration.
The flexible closure described above is located outdoors and serves to contain any leakage from the flued head so that the leakage is routed back to the annulus, and to seal the annulus from the outdoors.
Guides and anchors limit movement of pipes such that design limits on the containment penetration and bellows are not exceeded during plant operation, testing, or postulated accidents.
Penetration Type XXI The ERCW lines and several component cooling water lines employ penetration type XXI, as shown in Figure 6.2.4-17B. Process lines are welded directly to these penetrations.
Penetration Type XXII The type XXII penetration is used for the multiple line nitrogen penetration. This penetration is shown in Figure 6.2.4-17C.
Containment Isolation Systems 6.2.4-11
WATTS BAR WBNP-112 Penetration Type XXIII This type of penetration is used for the chilled water lines and each penetration contains a single chilled water line. The penetration is illustrated in Figure 6.2.4-17D.
Penetration Type XXIV Type XXIV penetrations are used for maintenance ports. These penetrations employ bellows as shown in Figure 6.2.4-17E. Any leakage through the flued heads or through the bellows will be into the annulus and thereby processed by the emergency gas treatment system.
The following codes, standards, and guides were applied in the design of the containment isolation system.
(1) 10 CFR Part 50 (2) ASME Boiler and Pressure Vessel Code Section III (3) Regulatory Guide 1.26 (4) Regulatory Guide 1.29 (5) ANSI N18.2-August 1970 draft (6) IEEE Standard 317-1976 6.2.4.3 Design Evaluation The containment isolation systems are designed to present a double barrier to any flow path from the inside to the outside of the containment using the double-barrier approach to meet the single-failure criterion.
When permitted by fluid system design, diverse modes of actuation are used for automatic isolation valves. In addition to diverse modes of operation, channel separation is also maintained. This also ensures that the single-failure criterion is met.
Adequate protection is provided for piping, valves, and vessels against dynamic effects and missiles which might result from plant equipment failures, including a LOCA.
Isolation valves inside the containment are located between the crane wall and the inside containment wall. The crane wall serves as the main missile barrier. Other missile barriers are discussed in Section 3.5.
The requirements and intent of NRC General Design Criteria 54, 55, 56, and 57 have been met with five exceptions.
(a) Primary containment monitoring instrument systems shall be designed to maintain the integrity of the containment isolation boundary in the event of a DBE. The instrument systems consist of pressure sensors (e.g., transmitters) located outside containment and associated sense 6.2.4-12 Containment Isolation Systems
WATTS BAR WBNP-112 lines that connect to the containment penetration nozzles. The sensors should be located as close as practical to the associated penetration nozzle. Any drain or test line used shall meet the double isolation barrier by use of two normally closed manual valves in series.
The instrument system shall be designed to Seismic Category I requirements and evaluated for effects of possible missiles, pipe whip, and jet impingement.
(b.1) The reactor vessel level indication system (RVLIS) is required post accident for continual indication of the water level in the reactor vessel.
The capillary sensing lines which transmit pressure from the reactor vessel to instruments in the Auxiliary Building are armored and designed to withstand DBE conditions. Any containment isolation valves installed in the RVLIS capillary lines will jeopardize the performance of the system. For this reason, isolation of these capillary lines is accomplished by a sealed sensor located inside containment and an isolator located outside containment. These devices utilize a type of bellows which transmits pressure while preventing mixing of the fluids on either side of the isolation devices. The capillary line is armored stainless steel tubing and is filled with demineralized water and sealed. A postulated shear of this capillary line on either side of the containment would not allow a leak to develop through the containment boundary.
(b.2) The RCS wide range pressure transmitter (PT-68-70) is required post accident for continual indication of the pressure in the reactor vessel.
The capillary sensing lines which transmit pressure from the reactor vessel to instruments in the Auxiliary Building are armored and designed to withstand DBE conditions. Any containment isolation valves installed in the RCS wide range pressure transmitter capillary lines will jeopardize the performance of the system. For this reason, isolation of these capillary lines is accomplished by a sealed sensor located inside containment and an isolator located outside containment.
These devices utilize a type of bellows which transmits pressure while preventing mixing of the fluids on either side of the steel tubing and is filled and sealed. A postulated shear of this capillary line on either side of the containment would not allow a leak to develop through the containment boundary.
(c) Containment isolation for each RHR sump line penetration consists of:
(1) A closed system outside containment.
(2) A containment isolation valve outside containment in each of the two lines after the penetrating line branches in the RHR sump valve room. Both of these valves are remotely controlled from the main control room.
Containment Isolation Systems 6.2.4-13
WATTS BAR WBNP-112 An enclosure of the RHR sump lines and isolation valves is provided from the containment out to and including the isolation valves.
However, this enclosure is not designed to be leaktight after an accident for the following reasons:
(1) The maximum pressure which will be experienced inside the RHR sump line will only be about 25 psig.
(2) One of the isolation valves, the containment sump valve, is qualified to 600 psig. The other isolation valve, the containment spray valve, is qualified to 200 psig.
(3) This portion of the system only operates post accident and, therefore, only a limited leak passive failure need be postulated (and this would be at the valve). However, based on the above two statements and the fact that deadweight loading (i.e., normal operation) should not exceed the MELB criteria, the over-design should preclude any problem.
Thus, the penetration has such overconservatism in its design that an external leaktight enclosure around the valves is not necessary.
(d) The pressure boundary valve leak rate test line containment isolation valves (63-158,63-112, 63-111,63-167, 63-174, 63-21, and 63-121) are remote manually actuated from the main control room and do not receive a containment isolation signal. These valves are open for short periods of time during normal operation for the performance of SIS and RHR system venting. Thus, these valves do not automatically close when the containment isolation or safety injection signal is initiated during the venting of the SIS and RHR system. This exception is acceptable because administrative controls exist in the test document to assure valve closure after testing and containment integrity is not compromised during pump operation (i.e., during testing at accident conditions) since flow is being maintained into containment.
(e) The design configuration for penetrations X-79A (ice blowing), and X-79B (negative return) is temporarily modified in operating Modes 5 and 6 and when the reactor is defueled to support ice blowing activities.
The normally closed blind flange on each penetration will be opened and temporary piping will be installed in the penetrations. A 12-inch silicone seal will be installed between the piping segment and the penetration. Manual isolation valves will be connected to the piping on the inboard and outboard side of the penetrations. Administrative controls will ensure timely closure of the valves, if necessary, subsequent to a LOCA in the other unit. The penetrations will be returned to their normal design configuration prior to entry into Mode 4 operations.
6.2.4-14 Containment Isolation Systems
WATTS BAR WBNP-112 6.2.4.3.1 Possible Leakage Paths Possible leakage paths from the containment are defined below. The leakage paths are defined on the basis that the annulus pressure is less than outdoor ambient, the Auxiliary Building, and the containment pressures. Therefore, whenever containment is required, leakage is into the annulus. The possible leakage paths considered do not include containment leakage through the steel plates or through the full penetration welds in the containment vessels. The possible leakage paths also do not include Shield Building embedments. This is acceptable, as leakage through any of these paths will be into the annulus and the leakage will be processed by the EGTS.
The more probable sources of containment and Shield Building leakage, such as elastomer seals, bellows, and through lines are considered as possible leak path types. Each penetration that contains elastomer seals or a bellows has at least one leakage path defined in Table 6.2.4-1. Penetrations not open to the annulus are considered as possible paths for through-line containment leakage and have one or more isolation valves. Thus every pipe penetration has at least one type of leak path listed in Table 6.2.4-1. The five different types of possible leakage paths are shown in Figure 6.2.4-20, tabulated in Table 6.2.4-1 and are discussed separately below.
Type A - Leakage Path Type A leakage is leakage from the Auxiliary Building into the annulus. Type A penetration leakage includes the following:
(1) Equipment hatch Shield Building sleeve leak (see Figure 6.2.4-12).
(2) Annulus access door leak.
(3) Containment purge supply and exhaust isolation valves outside Shield Building leak. The possible leakage is through the valves and the leakoff (see Figure 6.2.3-2) into the annulus.
(4) Shield Building penetration seal leakage.
Type B - Leakage Path Type B leakage paths are from the containment to the annulus. Type B leakage includes the following:
(1) Equipment hatch double O-ring through-line leak (see Figure 6.2.4-12).
(2) Ice blowing line O-ring and blind flange through line leak (see Figures 6.2.4-16 and 6.2.4-23).
(3) Penetration bellows leak.
(4) Containment purge supply and exhaust inboard and outboard valves through line leak. The leakage will pass through the leak off (see Figure 6.2.3-2) into the annulus.
Containment Isolation Systems 6.2.4-15
WATTS BAR WBNP-112 (5) Containment Incore Instrumentation Thimble Assembly renewal line double O-ring through-line leak (see Figure 6.2.4-15).
Type C - Leakage Path Type C leakage is leakage from the out-of-doors into the annulus and includes the following:
(1) Shield Building Incore Instrumentation Thimble Assembly renewal line through-line leak.
(2) Main steam and feedwater lines annulus seal leak.
(3) Ice blowing line Shield Building blind flange leak (See Figure 6.2.4-16).
Type D - Leakage Path Type D leakage path covers the through-line leakage from the containment to the Auxiliary Building (see Table 6.2.4-2). Included in this type of leakage are the lines associated with the safety systems required for post-LOCA operation, such as containment spray, RHR spray, high-head SIS, low-head SIS, SIS pump discharge, charging pump discharge, and containment emergency sump. For "closed" systems inside the Auxiliary Building, the through-line leakage will stay within the closed system. The component cooling water system is basically a closed system, except for the vent header at the surge tank. Any through-line leakage into the Auxiliary Building through this vent will be processed by the auxiliary building gas treatment system.
Radiation monitoring is provided as a signal to initiate the closing of the vent. The nitrogen supply lines to the pressurizer relief tank and to the accumulators are normally closed. The high pressure outside of the isolation valves serves to minimize through-line leakage outward. The personnel lock is yet another possible source for through-line leakage, but the leakage through the double O-ring (assuming one door open) is small, if any, and will be processed by the auxiliary building gas treatment system.
Type E - Leakage Path Type E leakage paths are paths from the containment that bypass the annulus and leak directly past a cleanup system. These leakage paths were considered during the design of the Watts Bar Nuclear Plant. The design features utilized at Watts Bar eliminates type E leakage paths. This is done by the following methods:
(1) Portions of the Auxiliary Building are maintained at a negative pressure relative to the outside atmosphere for the duration of an accident. Section 6.2.3 describes the implementing system and its operation.
(2) Leakoff lines to the secondary containment and a third outboard valve receiving an isolation signal are used in certain lines (such as the containment purge lines) to prevent bypass leakage.
6.2.4-16 Containment Isolation Systems
WATTS BAR WBNP-112 (3) A water seal(s) at greater than peak accident pressure or which has been shown by analysis to provide the necessary containment integrity is used to prevent bypass leakage in certain lines (such as the safety injection pump discharge or ERCW upper and lower compartment supply and return lines).
The seals are available for at least 30 days after a design basis event (see Table 6.2.6-3.
(4) The secondary side of the steam generator is kept at a higher pressure than the primary side soon after the LOCA occurs (see Section 10.4.3). Leakage between the primary and secondary sides of the steam generator is thus directed inward to the containment.
(5) For the maintenance ports through penetrations X-108 and X-109, a blind flange with a double O-ring design that is not opened during power operation and has a zero leakage acceptance criteria is relied upon to prevent bypass leakage.
Table 6.2.4-3 lists potential bypass leakage paths to the atmosphere and the methods chosen to eliminate such leakage.
6.2.4.4 Tests and Inspections Components of the containment isolation systems were designed, fabricated, and tested under quality assurance requirements in accordance with 10 CFR 50, Appendix B, as further described in Chapter 17. An alternative to visual examination during ASME Section III hydrostatic pressure testing was approved by Reference [1] for penetrations having inaccessible vendor welds.
Nondestructive examination was performed on the components of the system in accordance with the applicable codes described in Section 3.2.
Subsequent to initial plant operation, containment isolation systems are periodically tested under conditions of normal operation to determine that all systems are in constant readiness to perform the desired function.
Automatic isolation valves that receive a containment isolation signal to close, where closure of the valve will not limit or restrict normal plant operation, are periodically functionally tested by the on-line testing capability described in Section 7.3.1.1.3.
Other valves are periodically tested for CIS circuit electrical continuity. Other testing information is provided in Section 6.2.6.
REFERENCES (1) NRC Inspection Report Nos. 50-390/90-04 and 50-391/90-04, dated May 17, 1990.
Containment Isolation Systems 6.2.4-17
WATTS BAR WBNP-112 Table 6.2.4-1 Watts Bar Nuclear Plant Containment Penetrations And Barriers DUE TO THE SIZE OF TABLE 6.2.4-1 IT IS LOCATED IN THE OVERSIZED TABLE FILE 6.2.4-18 Containment Isolation Systems
Containment Isolation Systems WATTS BAR Table 6.2.4-1 Watts Bar Nuclear Plant Containment Penetrations And Barriers (Sheet 65 of 69)
ABBREVIATIONS FOR TABLE VALVE TYPE ACTUATORS ISOLATION SIGNAL GL = GLOBE AO = AIR OPERATED CV = CONTAINMENT VENT ISOLATION GA = GATE MO = MOTOR OPERATED PA = PHASE A BF = BUTTERFLY SO = SOLENOID OPERATED PB = PHASE B CK = CHECK M = MANUAL PR = PUMP RUN A = ANGLE CP = CONTAINMENT PRESSURE ILRT RV = RELIEF SI = SAFETY INFECTION C = CLOSED DI = DIAPHRAGM AFIS = AUXILIARY FEEDWATER ISOLATION O = OPEN SIGNAL BL = BLIND FLANGE MS = MAIN STEAM ISOLATION SIGNAL TC = TEST CONNECTION FW = FEEDWATER ISOLATION SIGNAL TO = TEST DRAIN TV = TEST VENT WV = WAFER VALVE D = DOOR BA = BALL PG = PLUG 6.2.4-19 WBNP-112
6.2.4-20 WATTS BAR Table 6.2.4-1 Watts Bar Nuclear Plant Containment Penetrations And Barriers (Sheet 66 of 69)
ABBREVIATIONS FOR TABLE ACTUATION MODE VALVE POSITIONS RM = REMOTE MANUAL O = OPEN LM = LOCAL MANUAL C = CLOSED SA = SELF ACTUATOR V = VARIES AT = AUTO TRIP AI = AS IS AO = AUTO OPEN LC = LOCKED CLOSED PROCESS FLUID STATE POSSIBLE LEAKAGE PATHS C = COLD SEE FSAR SECTION 6.2.4.3.1 H = HOT FLUID BUILDING STRUCTURES A = AIR CB = CONTAINMENT BUILDING Containment Isolation Systems W = WATER SB = SHIELD BUILDING S = STEAM AB = AUXILIARY BUILDING N = NITROGEN AEB = ADDITIONAL EQUIPMENT BUILDING WBNP-112 I = ICE G = GLYCOL
Containment Isolation Systems WATTS BAR Table 6.2.4-1 Watts Bar Nuclear Plant Containment Penetrations And Barriers (Sheet 67 of 69)
- 1. A DASH IS PRINTED IN DATA SPACES THAT DO NOT APPLY TO THE PENETRATION BEING DESCRIBED.
- 2. AN M AT THE END OF A CONTAINMENT OR SHIELD BUILDING PENETRATION NUMBER INDICATES THE PENETRATION HAS MORE THAN ONE LINE GOING THROUGH IT.
- 3. PIPING SYSTEMS ISOLATED BY A CONTAINMENT VENTILATION (CV) SIGNAL ARE ALSO ISOLATED BY A PHASE A SIGNAL.
- 4. PIPING INSIDE THE CONTAINMENT VESSEL HAS FIVE BRANCHES. IDENTICAL ISOLATION VALVES ARE INSTALLED IN EACH BRANCH. ONE VALVE IS NORMALLY OPEN. THREE OTHER VALVES ARE NORMALLY CLOSED AND ALSO RECEIVE PHASE A SIGNAL.
THE FIFTH VALVE IS A RELIEF VALVE WHICH RELIEVES INTO CONTAINMENT.
- 5. THE PIPING IS JOINED BY A LINE LEADING TO THE NITROGEN SUPPLY OUTSIDE OF THE SHIELD BUILDING. THIS LINE IS ISOLATED BY AN AIR OPERATED GATE VALVE WITH PHASE A ISOLATION.
- 6. DUCTING OUTSIDE THE SHIELD BUILDING HAS TWO BRANCHES. IDENTICAL SECONDARY CONTAINMENT ISOLATION VALVES ARE INSTALLED IN EACH BRANCH.
- 7. PIPING OUTSIDE OF THE SHIELD BUILDING HAS NINE BRANCHES. EACH LINE IS ISOLATED BY A RELIEF VALVE.
- 8. INSIDE THE CONTAINMENT VESSEL A LINE IS PROVIDED FOR PRESSURE RELIEF OF THE VOLUME BETWEEN THE ISOLATION VALVES. THIS LINE IS ISOLATED BY A CHECK VALVE.
- 9. THE PIPING IS JOINED BY A LINE USED FOR S.I.S. TESTING OUTSIDE OF THE SHIELD BUILDING. THIS LINE IS ISOLATED BY AN AIR OPERATED GLOBE VALVE WITH REMOTE MANUAL ACTUATION FROM THE MAIN CONTROL ROOM.
- 10. THE PIPING HAS A BYPASS LINE ATTACHED TO IT INSIDE THE ANNULUS. THIS BYPASS LINE IS ISOLATED BY A LOCKED CLOSED GATE VALVE WITH LOCAL MANUAL OPERATION.
- 11. ISOLATION INSIDE CONTAINMENT IS ACCOMPLISHED BY A CLOSED SYSTEM.
- 12. THE DP SENSORS ARE CLOSED SYSTEMS OUTSIDE OF CONTAINMENT THAT ARE ATTACHED DIRECTLY TO THE CONTAINMENT.
NO IN LINE ISOLATION VALVES ARE EMPLOYED FOR THESE SENSORS REFER TO SECTION 6.2.4.3.
6.2.4-21 WBNP-112
6.2.4-22 WATTS BAR Table 6.2.4-1 Watts Bar Nuclear Plant Containment Penetrations And Barriers (Sheet 68 of 69)
- 13. POST ACCIDENT MONITORING SYSTEM (PAMS) WIDE RANGE PRESSURE SENSORS ALSO MONITOR PRESSURE THROUGH THIS PENETRATION.
- 14. THE SECONDARY CONTAINMENT ISOLATION VALVE(S), WHICH REPRESENT AN ADDITIONAL BOUNDARY OUTSIDE CONTAINMENT IN HVAC SYSTEMS, ARE USED TO PREVENT BYPASS LEAKAGE FROM THE ANNULUS.
- 16. THE PRIMARY AND SECONDARY CONTAINMENT PENETRATIONS ARE NOT CONNECTED EXCEPT FOR THE TYPE A TEST PRESSURIZATION.
- 17. OUTSIDE CONTAINMENT, RELIEF VALVES RELEASE INTO THIS LINE IN THE EVENT OF SIS OVERPRESSURE, THUS THE SYSTEM IS ALMOST ALWAYS CLOSED, BUT COULD OPEN FOR PRESSURE RELIEF ANYTIME SIS IS ON.
- 18. OUTSIDE CONTAINMENT, A ONE INCH LINE TIES IN BETWEEN THE OUTER ISOLATION VALVE AND PRIMARY CONTAINMENT. THIS LINE IS ISOLATED BY A MANUALLY LOCKED CLOSED CONTAINMENT ISOLATION VALVE.
- 19. THE CONTAINMENT ISOLATION VALVES IN THIS LINE REQUIRE SIMULTANEOUS OPEN SIGNALS FROM TWO SEPARATE SWITCHES IN ORDER TO OPEN. ONE SWITCH IS LOCATED IN THE MAIN CONTROL ROOM AND THE OTHER IS LOCATED IN THE REMOTE SAMPLING STATION.
- 20. DELETED FOR UNIT 2.
- 21. THIS LINE TRANSMITS PRESSURE FROM THE PRIMARY COOLANT SYSTEM TO PRESSURE INSTRUMENTATION FOR DETERMINING THE REACTOR VESSEL FLUID LEVEL. THE LINE IS FLUID FILLED AND DOUBLE DIAPHRAGMED TO PREVENT COMMUNICATION BETWEEN THE PRIMARY SYSTEM FLUID AND THE AUXILIARY BUILDING. NO PRIMARY SYSTEM FLUID TRAVELS THROUGH THE Containment Isolation Systems PENETRATION SINCE THE INNER DIAPHRAGM IS LOCATED NEAR THE REACTOR VESSEL. SINCE DOUBLE DIAPHRAGMS ARE EMPLOYED FOR CONTAINMENT ISOLATION, NO CONTAINMENT ISOLATION VALVES ARE USED.
- 22. THIS LINE JOINS THE SECONDARY SIDE OF THE STEAM GENERATOR(S) INSIDE CONTAINMENT AND IS THEREFORE CONSIDERED A CLOSED SYSTEM INSIDE CONTAINMENT. THE ISOLATION VALVES WHICH EXIST OUTBOARD OF CONTAINMENT ARE NOT LEAKRATE TESTED DUE TO FLOODING OF THE STEAM GENERATORS POST LOCA.
WBNP-112
Containment Isolation Systems WATTS BAR Table 6.2.4-1 Watts Bar Nuclear Plant Containment Penetrations And Barriers (Sheet 69 of 69)
- 23. BETWEEN PRIMARY CONTAINMENT AND THE OUTER ISOLATION VALVE IN THIS LINE, AN AUXILIARY FEEDWATER LINE ADJOINS.
THE AUXILIARY FEEDWATER LINE HAS ISOLATION VALVES WHICH ARE ISOLATED IN THE SAME MANNER AS THE AUXILIARY FEEDWATER ISOLATION VALVES LISTED FOR X-40A AND X-40B.
- 24. NOT USED
- 25. AZIMUTH INFORMATION FOR THESE LINES CAN BE FOUND IN CHICAGO BRIDGE & IRON CO. STEEL CONTAINMENT VESSEL DATA PACKAGE (RIMS #B48850425301).
- 26. NO TYPE C LEAKAGE RATE TEST IS PERFORMED ON THIS LINE, BUT A WATER INVENTORY LEAKAGE RATE TEST IS PERFORMED ON THE MOV LOCATED OUTSIDE CONTAINMENT. THIS WATER LEAKAGE TEST ASSURES THAT THE WATER LEG, LOCATED IMMEDIATELY INBOARD OF THE MOV, WILL MAINTAIN A SUFFICIENT INVENTORY TO MAINTAIN A PRESSURE OF AT LEAST 1.1 TIMES THE MAXIMUM CALCULATED CONTAINMENT ACCIDENT PRESSURE ON THE MOV FOR 30 DAYS AFTER AN ACCIDENT.
- 27. PENETRATION X-118 IS OPENED BY REMOVING THE BLIND FLANGE IN THE ANNULUS TO ALLOW THE WATER WHICH HAS COLLECTED IN THE ANNULUS FROM LEAKAGE THROUGH THE PENETRATIONS OR SEEPAGE THROUGH THE CONCRETE TO DRAIN THE REACTOR BUILDING FLOOR AND EQUIPMENT DRAIN SUMP.
- 28. THIS LINE TRANSMITS PRESSURE FROM THE PRIMARY COOLANT SYSTEM TO PRESSURE INSTRUMENTATION. THE LINE IS FLUID FILLED AND DOUBLE DIAPHRAGMED TO PREVENT COMMUNICATION BETWEEN THE PRIMARY SYSTEM FLUID AND THE AUXILIARY BUILDING. NO PRIMARY SYSTEM FLUID TRAVELS THROUGH THE PENETRATION SINCE THE INNER DIAPHRAGM IS LOCATED NEAR THE REACTOR VESSEL. SINCE DOUBLE DIAPHRAGMS ARE EMPLOYED FOR CONTAINMENT ISOLATION, NO CONTAINMENT ISOLATION VALVES ARE USED.
- 29. SYS.26 HPFP LINE SUPPLIES THE CABLE TRAY INTERACTION (RB ANNULUS) THROUGH SHIELD BUILDING PEN. MK 103 LOCATED AT THE SAME EL AND AZ AS CONTAINMENT PEN.X-88 (REF.DWG. 47W850-9).
- 30. SYS.26 HPFP LINE SUPPLIES THE STAND PIPE (RB ANNULUS) THROUGH SHIELD BUILDING PEN. MK 104 LOCATED AT THE SAME EL AND AZ AS CONTAINMENT PEN.X-89 (REF.DWG. 47W850-9).
6.2.4-23 WBNP-112
Table 6.2.4-2 Possible Bypass Leakage Paths To The Auxiliary Building (Page 1 of 6) 6.2.4-24 WATTS BAR Penetration Number Penetrating Line Name Description X-2 A, B Personnel Access Hatch Any leakage would be treated by the ABGTS.
X-3 Fuel Transfer Tube Any leakage would be treated by the ABGTS.
X-15 Chemical and Volume Letdown Line Any leakage would be treated by the ABGTS.
X-16* Normal Charging Line High water pressure maintained on outboard valve, even in the event of a single failure.
X-17 RHR Hot Leg Injection System is in operation after an accident. Cross ties between pumps maintain flows in the event of a single failure.
X-19 A&B* RHR Sump Suction Line Line is always filled with water. No atmospheric bypass leakage to the Auxiliary Building can occur after a LOCA.
X-20 A&B* SIS RHR Pump Discharge System is in operation after a LOCA. Cross ties between pumps maintain flows and pressure in the event of a single failure.
X-21* Safety Injection Pump Discharge Line in use during a LOCA which will be pressurized even in the event of a single failure due to cross ties between pumps.
X-22* Charging Pump Discharge Same as for Penetration No. 21.
X-24* SIS Relief Valve Discharge Any leakage through the relief valve is prevented as the valves are pressurized Containment Isolation Systems outside containment by the SIS system. Any leakage would be into containment.
X-25A Pressurizer Liquid Sample Any leakage would be treated by the ABGTS.
X-25D Pressurizer Steam Sample Any leakage would be treated by the ABGTS.
WBNP-112 X-27 A, B, C, D Steam Generator Sample Lines Any leakage would be treated by the ABGTS.
Table 6.2.4-2 Possible Bypass Leakage Paths To The Auxiliary Building (Page 2 of 6)
Containment Isolation Systems WATTS BAR Penetration Number Penetrating Line Name Description X-29 CCS from RC Pump Coolers Any leakage would be treated by the ABGTS.
X-30 Accumulator to Holdup Tanks Any leakage would be treated by the ABGTS.
X-31 Fire Protection Any leakage would be treated by the ABGTS.
X-32* Safety Injection Discharge Same as for Penetration No. 21.
X-33* Safety Injection Discharge Same as for Penetration No. 21.
X-34 Control Air I&C Any leakage would be treated by the ABGTS.
X-35 CCS from Excess Letdown Heat Exchanger Same as for Penetration No. 29.
X-39A N2 to Accumulators Any leakage would be treated by the ABGTS.
X-39B N2 to Pressurizer Relief Tank Any leakage would be treated by the ABGTS.
X-40D Service Air Any leakage would be treated by the ABGTS.
X-41 Floor Sump Pump Discharge Any leakage would be treated by the ABGTS.
X-42 Pressurizer Relief Tank Makeup Any leakage would be treated by the ABGTS.
X-43 A*,B*,C*,D* To RC Pump Seals The line is pressurized during a LOCA even in the event of a single failure. If there was any leakage it would be treated by the ABGTS.
X-44 From RC Pump Seals Any leakage would be treated by the ABGTS.
X-45 RC Drain Tank and PRT to Vent Header Any leakage would be treated by the ABGTS.
X-46 RC Drain Tank Pump Discharge Any leakage would be treated by the ABGTS.
X-47A Glycol Line to Ice Condenser Any leakage would be treated by the ABGTS.
WBNP-112 X-47B Glycol Line from Ice Condenser Any leakage would be treated by the ABGTS.
6.2.4-25
Table 6.2.4-2 Possible Bypass Leakage Paths To The Auxiliary Building (Page 3 of 6) 6.2.4-26 WATTS BAR Penetration Number Penetrating Line Name Description X-48 A&B* Containment Spray System in operation after a LOCA. A 30-day water leg seal is maintained in this line.
X-49 A&B RHR Spray System in operation after a LOCA. System pressure maintained even in the event of a single failure due to pump cross ties.
X-50A RCP Thermal Barrier Return Same as for Penetration No. 29.
X-50B RCP Thermal Barrier Supply Any leakage would be treated by the ABGTS.
X-52* CCS to RC Pump Coolers Same as for Penetration No. 43.
X-53* CCS to Excess Letdown Heat Exchanger Same as for Penetration No. 43.
X-56A* Lower Containment ERCW Supply High water pressure maintained on outboard valve, even in the event of a single failure.
X-57A* Lower Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure.
X-58A* Lower Containment ERCW Supply High water pressure maintained on outboard valve, even in the event of a single failure.
X-58B RCS Pressure Sensor Any leakage would be treated by the ABGTS.
X-59A* Lower Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure.
Containment Isolation Systems X-60A* Lower Containment ERCW Supply High water pressure maintained on outboard valve, even in the event of a single failure.
X-61A* Lower Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure.
X-62A* Lower Containment ERCW Supply High water pressure maintained on outboard valve, even in the event of a WBNP-112 single failure.
X-63A* Lower Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure.
Table 6.2.4-2 Possible Bypass Leakage Paths To The Auxiliary Building (Page 4 of 6)
Containment Isolation Systems WATTS BAR Penetration Number Penetrating Line Name Description X-64 Inst. Rm, AC Chilled Water Return Any leakage would be treated by the ABGTS.
X-65 Inst. Rm. AC Chilled Water Supply Any leakage would be treated by the ABGTS.
X-66 Inst. Rm. AC Chilled Water Return Any leakage would be treated by the ABGTS.
X-67 Inst. Rm. AC Chilled Water Supply Any leakage would be treated by the ABGTS.
X-68* Upper Containment ERCW Supply High water pressure maintained on outboard valve, even in the event of a single failure.
X-69* Upper Containment ERCW Supply High water pressure maintained on outboard valve, even in the event of a single failure.
X-70* Upper Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure.
X-71* Upper Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure.
X-72* Upper Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure.
X-73* Upper Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure.
X-74* Upper Containment ERCW Return High water pressure maintained on outboard valve, even in the event of a single failure.
X-75* Upper Containment ERCW Supply High water pressure maintained on outboard valve, even in the event of a single failure.
X-76 Service Air Any leakage would be treated by the ABGTS.
X-77 Demineralized Water Any leakage would be treated by the ABGTS.
6.2.4-27 WBNP-112 X-78 Fire Protection Any leakage would be treated by the ABGTS.
Table 6.2.4-2 Possible Bypass Leakage Paths To The Auxiliary Building (Page 5 of 6) 6.2.4-28 WATTS BAR Penetration Number Penetrating Line Name Description X-81 RC Drain Tank to Gas Analyzer Any leakage would be treated by the ABGTS.
X-82 Refueling Cavity C-U Pump Suction Any leakage would be treated by the ABGTS.
X-83 Refueling Cavity C-U Pump Discharge Any leakage would be treated by the ABGTS.
X-84A Pressurizer Relief Tank to Gas Analyzer Any leakage would be treated by the ABGTS.
X-84B Reactor Vessel Level Indicating System Any leakage would be treated by the ABGTS.
X-84C Reactor Vessel Level Indicating System Any leakage would be treated by the ABGTS.
X-84D Reactor Vessel Level Indicating System Any leakage would be treated by the ABGTS.
X-85B Hot Leg Sample Any leakage would be treated by the ABGTS.
X-87B Reactor Vessel Level Indicating System Any leakage would be treated by the ABGTS.
X-87C Reactor Vessel Level Indicating System Any leakage would be treated by the ABGTS.
X-87D Reactor Vessel Level Indicating System Any leakage would be treated by the ABGTS.
X-90 Control Air Any leakage would be treated by the ABGTS.
X-91 Control Air Any leakage would be treated by the ABGTS.
Containment Isolation Systems WBNP-112
Table 6.2.4-2 Possible Bypass Leakage Paths To The Auxiliary Building (Page 6 of 6)
Containment Isolation Systems WATTS BAR Penetration Number Penetrating Line Name Description X-93 Accumulator Sample Any leakage would be treated by the ABGTS.
X-94 B, X-95 B Containment Atmosphere Radiation Monitor Any leakage would be treated by the ABGTS.
X-94 C, X-95 C Containment Atmosphere Radiation Monitor Any leakage would be treated by the ABGTS.
X-99 H2 Analyzer Any leakage would be treated by the ABGTS.
X-100 H2 Analyzer Any leakage would be treated by the ABGTS.
X-107 RHR Supply Any leakage would be treated by the ABGTS.
X-114 Ice Condenser (from Glycol Floor Cooling Coils) Any leakage would be treated by the ABGTS.
X-115 Ice Condenser (to Glycol Floor Cooling Coils) Any leakage would be treated by the ABGTS.
- Not a bypass leakage path to the Auxiliary Building.
6.2.4-29 WBNP-112
Table 6.2.4-3 Prevention Of Bypass Leakage To The Atmosphere (Page 1 of 2) 6.2.4-30 WATTS BAR Penetration Number Penetration Line Name Description X-4 Lower Compartment Purge Air Exhaust Leakoff lines to the annulus X-5 Instrument Room Purge Air Exhaust Leakoff lines to the annulus X-6 Upper Compartment Purge Air Exhaust Leakoff lines to the annulus X-7 Upper Compartment Purge Air Exhaust Leakoff lines to the annulus X-8A Feedwater Bypass Secondary side of the steam generator is pressurized above containment pressure X-8B Feedwater Bypass Same as for Penetration X-8A X-8C Feedwater Bypass Same as for Penetration X-8A X-8D Feedwater Bypass Same as for Penetration X-8A X-9A Upper Compartment Purge Air Supply Leakoff lines to the annulus X-9B Upper Compartment Purge Air Supply Leakoff lines to the annulus X-10A Lower Compartment Purge Air Supply Leakoff lines to the annulus X-10B Lower Compartment Purge Air Supply Leakoff lines to the annulus X-11 Instrument Room Purge Air Supply Leakoff lines to the annulus X-12A Feedwater Same as for Penetration X-8A X-12B Feedwater Same as for Penetration X-8A X-12C Feedwater Same as for Penetration X-8A X-12D Feedwater Same as for Penetration X-8A X-13A Main Steam Same as for Penetration X-8A X-13B Main Steam Same as for Penetration X-8A Containment Isolation Systems WBNP-112
Table 6.2.4-3 Prevention Of Bypass Leakage To The Atmosphere (Page 2 of 2)
Containment Isolation Systems WATTS BAR Penetration Number Penetration Line Name Description X-13C Main Steam Line Same as for Penetration X-8A X-13D Main Steam Line Same as for Penetration X-8A X-14A, B, C, D Steam Generator Blowdown Same as for Penetration X-8A X-40A Auxiliary Feedwater Same as for Penetration X-8A X-40B Auxiliary Feedwater Same as for Penetration X-8A X-56A Lower Compartment ERCW Supply Leakage prevented by combination of water seal and piping traps in conjunction with acceptance limits for Appendix J Testing as defined in design output.
X-57A Lower Compartment ERCW Return Same as for Penetration X-56A X-58A Lower Compartment ERCW Supply Same as for Penetration X-56A X-59A Lower Compartment ERCW Return Same as for Penetration X-56A X-60A Lower Compartment ERCW Supply Same as for Penetration X-56A X-61A Lower Compartment ERCW Return Same as for Penetration X-56A X-62A Lower Compartment ERCW Supply Same as for Penetration X-56A X-63A Lower Compartment ERCW Return Same as for Penetration X-56A X-68 Upper Compartment ERCW Supply Same as for Penetration X-56A X-69 Upper Compartment ERCW Supply Same as for Penetration X-56A X-70 Upper Compartment ERCW Return Same as for Penetration X-56A X-71 Upper Compartment ERCW Return Same as for Penetration X-56A X-72 Upper Compartment ERCW Return Same as for Penetration X-56A X-73 Upper Compartment ERCW Return Same as for Penetration X-56A X-74 Upper Compartment ERCW Supply Same as for Penetration X-56A X-75 Upper Compartment ERCW Supply Same as for Penetration X-56A X-80 Lower Compartment Pressure Relief Leakoff lines to the annulus X-108 Maintenance Port Blind Flange, double O-ring design with a zero leakage criteria; not open during power operation X-109 Maintenance Port Blind flange, double O-ring design with a zero leakage criteria; not open during power WBNP-112 operation 6.2.4-31
Table 6.2.4-4 Instrument Lines Penetrating Primary Containment (Page 1 of 3) 6.2.4-32 WATTS BAR Inner Outer Line Isolation Isolation Penetration Size Valve Valve Valve Valve Valve Valve Line Identification No. Number Inches Orifice Number Type Location Number Type Location Pressurizer Liquid 1 X-25A 3/8 No 43-11 Globe Inside Prim 43-12 Globe Annulus Sample Containment Pressurizer Steam 2 X-25D 3/8 No 43-2 Globe Inside Prim 43-3 Globe Annulus Sample Containment dP Sensor1 3 X-26C 1/2 No - - - - - -
Steam Generator 4 X-27A 3/8 No 43-54D Globe Inside Prim 43-55 Globe Annulus No. 1 Sample and Water Containment Quality Steam Generator 5 X-27B 3/8 No 43-56D Globe Inside Prim 43-58 Globe Annulus No. 2 Sample Containment Steam Generator 6 X-27C 3/8 No 43-59D Globe Inside Prim 43-61 Globe Annulus No. 3 Sample Containment Steam Generator 7 X-27D 3/8 No 43-63D Globe Inside Prim 43-64 Globe Annulus No. 4 Sample Containment dP Sensor1 X-57B 1/2 No - - - - - -
dP Sensor1 X-60B 1/2 No - - - - - -
dP Sensor1 X-102 1/2 No - - - - - -
Containment Isolation Systems WBNP-112
Table 6.2.4-4 Instrument Lines Penetrating Primary Containment (Page 2 of 3)
Containment Isolation Systems WATTS BAR Inner Outer Line Isolation Isolation Penetration Size Valve Valve Valve Valve Valve Valve Line Identification No. Number Inches Orifice Number Type Location Number Type Location Accum. to Holdup Tanks 8 X-30 3/4 No 63-071 Globe Inside Prim 63-084 Globe Outside Shield Containment Building Pressurizer Relief 9 X-84A 3/8 No 68-308 Globe Inside Prim 68-307 Globe Annulus Tank to Gas Analyzer Containment Reactor Vessel Level 10 X-84B 3/16 No - - - - - -
Ind Sys Reactor Vessel Level 11 X-84C 3/16 No - - - - - -
Ind Sys Reactor Vessel Level 12 X-84D 3/16 No - - - - - -
Ind Sys Hot Leg Sample - Loops 13 X-85B 3/8 No 43-22 Globe Inside Prim 43-23 Globe 1 and 3 Containment Reactor Vessel Level 16 X-87B 3/16 No - - - -
Ind Sys 6.2.4-33 WBNP-112
Table 6.2.4-4 Instrument Lines Penetrating Primary Containment (Page 3 of 3) 6.2.4-34 WATTS BAR Inner Outer Line Isolation Isolation Penetration Size Valve Valve Valve Valve Valve Valve Line Identification No. Number Inches Orifice Number Type Location Number Type Location Reactor Vessel Level 17 X-87C 3/16 No - - - - - -
Ind Sys Reactor Vessel Level 18 X-87D 3/16 No - - - - - -
Ind Sys Accumulator Sample 19 X-93 3/8 No 43-34 Globe Inside Prim Globe Annulus Containment 43-35 Lower Compartment 20 X-94B 1-1/2 No 90-110 Globe Inside Prim 90-111 Globe Annulus Air Monitor Intake Containment 90-108 90-107 Lower Compartment 21 X-94C 1-1/2 No 90-109 Globe Inside Prim Globe Annulus Air Monitor Return Containment Upper Compartment 22 X-95B 1-1/2 No 90-116 Globe Inside Prim 90-117 Globe Annulus Air Monitor Intake Containment Upper Compartment 23 X-95C 1-1/2 No 90-114 Globe Inside Prim 90-113 Globe Annulus Air Monitor Return 90-115 Containment Containment dP Sensor1 24 X-97 1/2 No - - - - - -
(PdT-30-133)
Containment dP Sensor1 25 X-98 1/2 No - - - - - -
(PdT-30-30C)
Hydrogen Analyzer 26 X-99 3/8 No 43-202 Globe Inside Prim.43-434 Globe Annulus Containment Isolation Systems Containment Hydrogen Analyzer 27 X-100 3/8 No 43-201 Globe Inside Prim.43-433 Globe Annulus Containment WBNP-112 1
These have no in-line containment isolation valves - see Section 6.2.4.3 and Table 6.2.4-1.
WATTS BAR Containment Isolation Systems Figure 6.2.4-1 Type 1, Main Steam X-l3A, X-l3B, X-l3C, X-13D WBNP-112 6.2.4-35
6.2.4-36 WATTS BAR Figure 6.2.4-2 Type II, Feedwater X-12A, X-l2B, X-12C, X-12D WBNP-112 Containment Isolation Systems
WATTS BAR Containment Isolation Systems Figure 6.2.4-3 Type III, Residual Heat Removal Pump Return X-17, Pump Supply X-I07 WBNP-112 6.2.4-37
6.2.4-38 WATTS BAR Figure 6.2.4-4 Type IV and V (Type IV Socket Weld Ends, Type V Butt Weld Ends)
WBNP-112 Containment Isolation Systems
WATTS BAR Containment Isolation Systems Figure 6.2.4-5 Type VI and VII (Type VI for Socket Weld SS Process Lines, Type 6.2.4-39 VII for Butt Weld SS Process Lines) WBNP-112
WATTS BAR WBNP-112 Figure 6.2.4-6 Type VIII, for Butt Weld C.S. Process Lines 6.2.4-40 Containment Isolation Systems
WATTS BAR WBNP-112 Figure 6.2.4-7 Type IX, for SS Process Lines Containment Isolation Systems 6.2.4-41
WATTS BAR WBNP-112 Figure 6.2.4-8 Type X, Instrument Penetrations 6.2.4-42 Containment Isolation Systems
WATTS BAR WBNP-112 Figure 6.2.4-9 Type XII, Emergency Sump Containment Isolation Systems 6.2.4-43
WATTS BAR WBNP-112 Figure 6.2.4-10 Type XI, Emergency Sump 6.2.4-44 Containment Isolation Systems
WATTS BAR WBNP-112 Figure 6.2.4-11 Type XIII, Ventilation Duct Penetration Containment Isolation Systems 6.2.4-45
WATTS BAR WBNP-112 Figure 6.2.4-12 Type XIV, Equipment Hatch 6.2.4-46 Containment Isolation Systems
WATTS BAR WBNP-112 Figure 6.2.4-13 Type XV, Personnel Access Containment Isolation Systems 6.2.4-47
WATTS BAR WBNP-112 Figure 6.2.4-14 Type XVI, Transfer Tube 6.2.4-48 Containment Isolation Systems
WATTS BAR WBNP-112 Figure 6.2.4-15 Type XVII, Incore Instrumentation Thimble Assembly Renewal Line Containment Isolation Systems 6.2.4-49
WATTS BAR WBNP-112 Figure 6.2.4-16 Type XVIII, Ice Blowing Line 6.2.4-50 Containment Isolation Systems
WATTS BAR WBNP-112 Figure 6.2.4-17 Type XIX, Electrical Penetration Containment Isolation Systems 6.2.4-51
6.2.4-52 WATTS BAR Figure 6.2.4-17A Type XX Feedwater Bypass Penetrations X-8A, X-8B, X-8C, X-8D WBNP-112 Containment Isolation Systems
WATTS BAR WBNP-112 Figure 6.2.4-17B Type XXI, Upper And Lower Containment ERCW Supply And Return CCW From Excess Letdown Heat Exchanger and from Pump Odolers Containment Isolation Systems 6.2.4-53
WATTS BAR WBNP-112 Figure 6.2.4-17C Type XXII Multi Line Penetration X-39 6.2.4-54 Containment Isolation Systems
WATTS BAR Containment Isolation Systems Figure 6.2.4-17D Type XXIII Instrument Room Chilled H20 Supply and Return WBNP-112 6.2.4-55
WATTS BAR WBNP-112 Figure 6.2.4-17E Type XXIV UHI X-l08, X-109 6.2.4-56 Containment Isolation Systems
WATTS BAR WBNP-112 Figure 6.2.4-18 Mechanical Containment Penetration Containment Isolation Systems 6.2.4-57
6.2.4-58 WATTS BAR Figure 6.2.4-19 Powerhouse Reactor Building Unit 1 & 2 Mechanical Sleeves-Shield Building WBNP-112 Containment Isolation Systems
WATTS BAR WBNP-112 Figure 6.2.4-20 Schematic Diagram of Leakage Paths Containment Isolation Systems 6.2.4-59
6.2.4-60 WATTS BAR Figure 6.2.4-21 Electrical Logic Diagram Containment Isolation WBNP-112 Containment Isolation Systems
WATTS BAR WBNP-112 Figure 6.2.4-22A through 6.2.4-22II Deleted by Amendment 65 Containment Isolation Systems 6.2.4-61
6.2.4-62 WATTS BAR Figure 6.2.4-23 Ice Blowing and Negative Return Lines - Blind Flange Details WBNP-112 Containment Isolation Systems
WATTS BAR WBNP-112 6.2.5 Combustible Gas Control in Containment The containment combustible gas control system is designed to control the concentration of hydrogen that may be released into the containment following a beyond-design-basis accident to ensure that containment structural integrity is maintained. The combustible gas control system consists of the containment air return system, the hydrogen analyzer system (HAS) and the hydrogen mitigation system (HMS) which conform to 10 CFR 50.44 requirements.
6.2.5.1 Design Bases In an accident more severe than the design-basis loss-of-coolant accident, combustible gas is predominantly generated within containment as a result of the following:
(1) Fuel clad-coolant reaction between the fuel cladding and the reactor coolant.
(2) Molten core-concrete interaction in a severe core melt sequence with a failed reactor vessel.
If a sufficient amount of combustible gas is generated, it may react with the oxygen present in the containment at a rate rapid enough to lead to a containment breach or a leakage rate in excess of Technical Specification limits. Additionally, damage to systems and components essential to continued control of the post-accident conditions could occur.
The systems provided for combustible gas control have the following functional and mechanical requirements:
(1) The air return fans enhance the ice condenser and containment spray heat removal operation by circulating air from the upper compartment to the lower compartment through the ice condenser, and then back to the upper compartment. Hydrogen concentration is limited in potentially stagnant regions by providing air flow in these regions.
(2) The HAS provides the capability for extracting a sample and obtaining the measurement necessary to determine the volume percent concentration for hydrogen present in the sample. The system provides indication and alarms of volume percent concentrations in the main control room. Indication is also provided at the remote control center.
(3) The HMS is designed to increase the containment capability to accommodate hydrogen that could be released during a degraged core accident. The system is based on the concept of controlled ignition using thermal igniters.
(4) The air return fans and HAS are designed to operate continuously during accident conditions. The HMS igniter assemblies are qualified for a 30 year life of operational cycles.
Combustible Gas Control in Containment 6.2.5-1
WATTS BAR WBNP-112 (5) The combustible gas control system is designed for periodic testing and inspection.
6.2.5.2 System Design Containment Air Return System Mixing of the containment atmosphere is accomplished by the containment air return system described in Section 6.8. The air return fans start automatically 9 + 1 minutes after receipt of a containment Phase B isolation signal (see 7.3.1.1.1). In addition, the fans may be started manually.
The associated ductwork, which must remain intact following a beyond-design-basis accident to assure that no localized hydrogen concentration exceeds 4%, consists of (1) two 12-inch ducts (one associated with each air return fan intake) which draw air from the containment dome region, (2) one 8-inch duct which circles the containment removing air from accumulator rooms and other dead-ended spaces and terminates at each air return fan housing, (3) two 12-inch ducts which circle the crane wall, removing air from the steam generator and pressurizer compartments and terminate through two 8-inch ducts at each air return fan housing, (4) two 8-inch pipes (one connected to each air return fan housing) which remove air from the refueling canal, and (5) the main duct between upper and lower compartment through the divider deck, including the non-return dampers.
The ductwork described above is embedded in concrete, where possible, to prevent damage from buildup of pressure during a beyond-design-basis accident. Ductwork not protected by embedment is also designed to withstand the beyond-design-basis accident environment. The air return system also includes heavy-duty backdraft dampers to prevent back flow from the lower compartment to the upper compartment under a differential pressure of 15 psig. These dampers prevent steam from bypassing the ice condenser during the initial blowdown. Figures 6.2.5-3, 6.2.5-4 and 6.2.5-5 are provided to show the routing of the recirculation ducts.
During the post-blowdown period, the pressure gradient between containment compartments is almost nonexistent and hydrogen can accumulate in potentially stagnant regions. The regions of concern are the ten dead-ended compartments: the four steam generator enclosures; the pressurizer enclosure; the four accumulator spaces; and the instrument room. The air return fans provide recirculation flow through the dead-ended compartments to prevent excessive hydrogen buildup. Each fan will mix 1,960 cfm form the enclosed areas in the lower compartment to the general lower compartment atmosphere.
Hydrogen Analyzer The HAS provides the capability to extract air samples from containment and to determine volume percent concentration of hydrogen. The primary functions of the system include continuous sampling from a remote location, measurement of hydrogen partial pressure, visual indication of volume percent concentrations and hydrogen concentration alarms in the main control room.
6.2.5-2 Combustible Gas Control in Containment
WATTS BAR WBNP-112 The sampling system consists of a single, non-trained detection loop. The analyzer is fed by one process sample line and returns to containment on one process effluent line. This line is equipped with two manually controlled isolation valves on both the sample and return lines. The system is installed at two locations. The sample loop station, mounted inside the Annulus, consists of the detection chamber, pressure transducer, solenoid valves, condensate management components and check valves for directing sample through the loop.
The HAS remote control center is mounted is a mild environment in the Auxiliary Building where access is always permitted. The major components of the center include a PLC based signal conditioner/system controller, a remote touch screen display and the system switch panel.
Containment isolation valve hand switches, a fan control hand switch, a hydrogen concentration indicator and alarms are provided in the main control room.
Upon actuation of the system, sample enters the loop assembly and passes through a T which separates the liquid and collects it in a condensate trap. The sample continues through a flow switch into the detection chamber. Inside the detection chamber, partial and total pressure measurements are obtained. The sample exits the detection chamber, passing through the sample pump which then drives the sample out of the loop assembly.
The analyzer is designed to continually measure hydrogen concentration following a beyond-design-basis accident. The analyzer is calibrated to measure hydrogen concentrations between zero and ten percent with an accuracy of +0.2% hydrogen. A sample loop flow diagram is shown in Figure 6.2.5-6.
The hydrogen analyzer components are seismically supported.
Hydrogen Mitigation System To assure that any hydrogen release would be ignited at containment locations as soon as the concentration exceeded the lower flammability limit, durable thermal igniters, capable of maintaining an adequate surface temperature, are used. An igniter developed by Tayco Engineering, operating at a nominal plant voltage of 120V AC, is used. The igniter has been shown by experiment to be capable of maintaining surface temperatures in excess of the required minimum for extended periods, initiating combustion and continuing to operate in various combustion environments.
The igniters in the HMS are equally divided into two redundant groups, each with independent and separate controls, power supplies and locations, to ensure adequate coverage even in the event of a single failure. Manual control of each group of igniters is provided in the main control room and the status (on-off) of each group is indicated there. A separate train of Class IE 480V AC auxiliary power is provided for each group of igniters and is backed by automatic loading onto the diesel generators upon loss of offsite power. Each individual circuit powers two igniters. See Figures 6.2.5-8 through 6.2.5-12 for igniter locations.
Combustible Gas Control in Containment 6.2.5-3
WATTS BAR WBNP-112 To assure adequate spatial coverage, 68 igniters are distributed throughout the various regions of the containment in which hydrogen could be released or to which it could flow in significant quantities (see Figures 6.2.5-8 through 6.2.5-12). There are at least two igniters, controlled and powered redundantly located in each of these regions. Following a degraded core accident, any hydrogen which is produced is released into the lower compartment inside the crane wall. To cover this region, 22 igniters (equally divided between trains) are provided. Eight of these are distributed on the reactor cavity wall exterior and crane wall interior at an intermediate elevation to ensure the partial burning that accompanies upward flame propagation.
Two igniters are located at the lower edge of each of the five enclosures for the four steam generators and the pressurizer, two in the top of the pressurizer enclosure and another pair above the reactor vessel in the cavity. These 22 lower compartment igniters help prevent flammable mixtures from entering the ice condenser. Any hydrogen not burned in the lower compartment is carried up through the ice condenser and into its upper plenum. Since steam is removed from the mixture as it is passed through the ice bed, mixtures that were nonflammable in the lower compartment tend to be flammable in the ice condenser upper plenum. This phenomenon is supported by the CLASIX containment analysis code which predicts more sequential burns to occur in the upper plenum than in any other region. Four igniters are located around the upper compartment dome, four at intermediate elevations on the outside of the steam generator enclosures, four more around the top inside of the crane wall and on above each of the two air return fans. The air return fans provide recirculation flow from the upper compartment through several dead-ended compartments (see Section 6.2.1.3.3) back into the main part of the lower compartment. To cover this region, there are pairs of igniters in each of the eight rooms (a total of 16 igniters) through which the recirculation flow passes. The location of the HMS igniters is shown in Figures 6.2.5-8 through 6.2.5-12.
The components of the HMS inside containment are seismically supported.
6.2.5.3 Design Evaluation Containment pressure during the post blowdown phase of a loss-of-coolant accident is calculated with the LOTIC code which models the containment structural heat sinks and containment safeguards system. The long-term containment pressure analysis accounts for hydrogen partial pressure. This transient is discussed in Section 6.2.1 and 15.4.1.2.
The containment air return system is designed to reduce containment pressure after blowdown to prevent excessive hydrogen concentrations in pocketed areas, and circulate air through the ice condenser. The air return fans automatically start on a Phase B containment isolation signal and can be started manually. The fans provide a continuous mixing of the containment compartment atmosphere for the long-term post-blowdown environment. The system has redundancy, is single-failure-proof and will remain operable with a loss of onsite or offsite power.
The hydrogen analyzer is a highly reliable commerical grade, Category 3 instrument as defined in Regulatory Guide 1.97 and permitted by Regulatory Guide 1.7. The 6.2.5-4 Combustible Gas Control in Containment
WATTS BAR WBNP-112 system is capable of being energized and fully operational within 90 minutes. It is required to operate correctly and continuously following a beyond-design-basis accident.
The HMS, due to its igniter type and locations, redundancy, capability of functioning in a post-accident environment, seismic support, main control room actuation, and remote surviellance, performs its intended function in a manner that provides adequate safety margins. The Unit 2 containment structures can survive the effects of credible degraded core accidents when hydrogen hazards are mitigated by HMS.
6.2.5.4 Testing and Inspections The combustible gas control system is subjected to periodic testing and inspection to demonstrate its availability.
The periodic test program for the containment air return system and the HMS are described in the Technical Specifications.
The periodic test program for the HAS is described in the Technical Requirements Manual.
Preoperational tests are described in Chapter 14.
6.2.5.5 Instrumentation Application The instrumentation design details of the air return fans are shown on Figures 9.4-30 and 9.4-33. The logic, controls and instrumentation of this engineered safety feature system are such that a single failure of any component does not result in the loss of functional capability for the system.
The HAS instrument range is configured to measure from 0-10% hydrogen by volume.
There are two configurable hydrogen concentration alarms, one on the remote control center and one in the main control room. The HAS also provides a trouble alarm to indicate failures of the sensor and pump. An equipment status display monitors pump pressure and flow.
Annunciation is provided in the main control room upon loss of power or undervoltage to the igniters. Each of the two HMS groups is placed in service from the main control room by a handswitch. The igniters are manually energized following any accident which indicates inadequate core cooling. This is done without waiting for a potential hydrogen buildup.
Combustible Gas Control in Containment 6.2.5-5
WATTS BAR WBNP-112 THIS PAGE INTENTIONALLY BLANK 6.2.5-6 Combustible Gas Control in Containment
WATTS BAR WBNP-112 Figure 6.2.5-1 Deleted by Amendment 95 Combustible Gas Control in Containment 6.2.5-7
WATTS BAR WBNP-112 Figure 6.2.5-2 Deleted By Amendment 62 6.2.5-8 Combustible Gas Control in Containment
WATTS BAR Combustible Gas Control in Containment Figure 6.2.5-3 Powerhouse Reactor Building Units 1 & 2 - Mechanical Heating, Ventilating and Air Conditioning WBNP-112 6.2.5-9
6.2.5-10 WATTS BAR Figure 6.2.5-4 Powerhouse Reactor Building Units 1 & 2 - Mechanical Heating, Ventilating and Air Conditioning WBNP-112 Combustible Gas Control in Containment
WATTS BAR Combustible Gas Control in Containment Figure 6.2.5-5 Powerhouse Reactor Building Units 1 & 2 - Mechanical Heating, Ventilation and Air Conditioning WBNP-112 6.2.5-11
WATTS BAR WBNP-112 Figure 6.2.5-6 Sample Loop Flow Diagram 6.2.5-12 Combustible Gas Control in Containment
WATTS BAR WBNP-112 Figure 6.2.5-7 Deleted by Amendment 95 Combustible Gas Control in Containment 6.2.5-13
WATTS BAR WBNP-112 Figure 6.2.5-7a Deleted by Amendment 95 6.2.5-14 Combustible Gas Control in Containment
WATTS BAR WBNP-112 Figure 6.2.5-8 Igniter Locations - Lower Compartment and Dead Ended Compartments Combustible Gas Control in Containment 6.2.5-15
WATTS BAR WBNP-112 Figure 6.2.5-9 Igniter Locations - Lower Compartments 6.2.5-16 Combustible Gas Control in Containment
WATTS BAR WBNP-112 Figure 6.2.5-10 Igniter Locations - Upper Plenum and Upper Compartments Combustible Gas Control in Containment 6.2.5-17
WATTS BAR WBNP-112 Figure 6.2.5-11 Igniter Locations - Dome 6.2.5-18 Combustible Gas Control in Containment
WATTS BAR WBNP-112 Figure 6.2.5-12 Igniter Locations - Elevation Combustible Gas Control in Containment 6.2.5-19
WATTS BAR WBNP-112 THIS PAGE INTENTIONALLY BLANK 6.2.5-20 Combustible Gas Control in Containment
WATTS BAR WBNP-112 6.2.6 Containment Leakage Testing Primary containment leakage tests and containment isolation system valve operability tests will be performed periodically to verify that leakage from the containment is maintained within acceptable limits set forth in the Technical Specifications. The types of leakage tests are as follows:
(1) Test Type A Tests to measure the reactor primary containment overall integrated leakage rate. The containment leak rate test will be conducted in accordance with 10 CFR 50, Appendix J, Option B.
(2) Test Type B Tests to detect and measure local leaks of containment penetrations, hatches, and personnel locks as required by 10 CFR 50, Appendix J, Option B.
(3) Test Type C Test to detect and measure containment isolation valve leakage as described by 10 CFR 50, Appendix J, Option B.
The leakage rate testing pressure for the above tests, Pa (as defined in 10CFR50 Appendix J), has a nominal value of 15.0 psig with allowance for instrument error.
Exceptions to this test pressure are noted elsewhere in this section.
6.2.6.1 Containment Integrated Leak Rate Test The maximum allowable containment leakage rate for the Watts Bar Nuclear Plant is 0.25 weight percent per day as specified in the Technical Specifications. The preoperational testing will be conducted in full compliance with 10 CFR 50, Appendix J as shown in Table 14.2-1. Subsequent periodic testing will also be performed in accordance with Appendix J, Option B with approved exemptions.
Prior to conducting the integrated leak rate test, those lines which penetrate primary containment are aligned as shown in Table 6.2.6-4.
The containment is then pressurized in accordance with 10 CFR 50, Appendix J, and the Technical Specification requirements. When test pressure is reached, the containment is isolated from its pressure source and the following parameters are recorded at periodic intervals:
(1) Containment absolute pressure (2) Dry bulb temperatures (3) Water vapor pressures Containment Leakage Testing 6.2.6-1
WATTS BAR WBNP-112 (4) Outside containment pressure and temperature conditions During the test, ventilation inside the containment is operated as necessary to enhance an even air temperature distribution. The test data are processed at periodic intervals during the test to determine test status and leakage conditions. If it appears that the leakage is excessive, the pressure plateau is either maintained on the test or aborted to perform repairs. The test is run for a prescribed time period to obtain assurance of the test leak rate.
Following the leak rate test, a second leak rate is performed to verify the information obtained in the first test. This verification test consists of slowly bleeding off pressure from containment at a known rate and measuring the total containment leak rate. The superimposed, measured flow is adjusted to a value which causes a change in the weight of air in the containment that is in the same order of magnitude as the allowable leakage rate.
The mass point equations are used to determine the integrated leak rate. The mass point equations will be used for preoperational testing as discussed in Table 14.2-1.
6.2.6.2 Containment Penetration Leakage Rate Test Table 6.2.4-1 lists penetrations in the primary containment. The Type B test is performed on all operational electrical equipment and personnel hatch, fuel transfer tube, Incore Instrumentation Thimble Assembly renewal and ice blowing penetrations, and penetration bellows in accordance with 10 CFR 50, Appendix J, Option B. The dual-ply bellows on containment penetration will be tested at Pa by applying the pressure between the plies. Airlock door seals are tested at 6.0 psig per Technical Specification requirements. Experience has shown that pressurizing the space between the seals to greater than 6.5 psig on personnel airlock doors of the design used at Watts Bar will lift the door and induce gross leakage unless strongbacks are used. Since the door seal test is intended to prove integrity of the seals, it is our position that a test conducted at 6.0 psig will conservatively demonstrate that seal integrity is maintained.
Table 6.2.6-1 lists all penetrations subjected to type B testing. Spare electrical penetrations will be subjected to Type B testing as they become operational. Tables 6.2.4-1 through 6.2.4-4 and Figures 8.3-44 and 8.3-45 give details on these penetrations. The test is performed in full compliance with 10 CFR 50, Appendix J, Option B. The acceptance criteria as required by Appendix J,Option B are specified in the Technical Specifications.
Table 6.2.4-1 lists containment isolation valves. Table 6.2.6-2 identifies those valves that are tested during a Type C test.
Isolation valves that are part of closed systems that are in use after a design basis event and valves that are water sealed for at least 30 days after a design basis event are not tested in the Type C test program (References 1, 2, and 3). Table 6.2.6-3 lists the valves exempted from type C leak testing. Bases for exemptions and exceptions from type C leakage rate testing on a penetration by penetration basis are as follows:
6.2.6-2 Containment Leakage Testing
WATTS BAR WBNP-112 (I) Exemptions (1) Feedwater Bypass - X-8A, X-8B, X-8C, X-8D Feedwater - X-12A, X-12B, X-12C, X-12D Main Steam - X-13A, X-13B, X-13C, X-13D Steam Generator Blowdown - X-14A, X-14B, X-14C, X-14D Steam Generator Blowdown sample line - X-27A, X-27B, X-27C, X-27D Auxiliary Feedwater, X-40A, X-40B These penetrations are directly connected to the secondary side of the steam generator. The main steam and feedwater lines of PWR containments are not required to be Type C tested (see definition of Type C test in 10 CFR 50, Appendix J). These lines are assumed not to rupture as a result of an accident (missile protected). Any leakage through these lines would be identified during operation by the leakage detection program. In addition, during a design basis accident, the secondary side of the steam generator is filled with water and would be at a higher pressure than the containment atmosphere thus preventing outleakage from containment. The integrity of the inside piping is also verified during the Type A test.
(2) CVCS Normal Charging Line, X-16 This penetration uses an inboard check valve and a closed loop outside containment (CLOC) as the means of containment isolation. Type C testing for this path is not required due to the seal pressure greater than 1.1 Pa and the 30-day water seal inventory. A positive pressure preventing air outleakage is assured by the pressure applied against FCV-62-90 and FCV-62-91 (both of which receive a safety injection signal to close) by the high head SI pumps. Water testing for piping integrity is performed in accordance with ASME XI.
(3) RHR Hot Leg Injection, X-17 This penetration uses inboard containment isolation valves and a CLOC for containment boundaries. Type C testing for this penetration is not required since a continuous water seal will be provided at a pressure greater than 1.1 Pa and a 30-day water seal is provided. Water testing for piping integrity is performed in accordance with ASME XI.
(4) RHR Pump Discharge, X-20A, X-20B Same as for X-17.
Containment Leakage Testing 6.2.6-3
WATTS BAR WBNP-112 (5) SIS Pump Discharge to Hot Leg Injection, X-21, X-32 These lines make use of inboard containment isolation valves and a CLOC for containment boundaries. These lines are postulated to be in-service post accident and the high head pumps will maintain a pressure seal greater than 1.1 Pa for greater than 30 days.
(6) Charging Pump Discharge, X-22 This line makes use of inboard containment isolation valves and a CLOC for containment boundaries. Type C testing is not required for the same reasons as X-21 and X-32. Water seal is provided by the high head pumps.
(7) SIS to Low Head SI, X-33 Same as X-21 and X-32 (8) RCP Seal Injection, X-43A, X-43B, X-43C, X-43D These lines made use of an inboard containment isolation valve and a CLOC for containment boundaries. Type C test is not required for the same reason as given for X-16.
(II) Exceptions (1) Sump Suction to RHR, X-19A, X-19B These lines make use of a containment isolation valve located outside of containment and a CLOC for containment isolation boundaries. During a design basis accident, these lines would be submerged under water which would preclude air outleakage. In addition, these valves are exposed to Pa during each Type A test.
(2) Relief Valve Discharge, X-24 The line uses an inboard containment isolation valve and a CLOC for containment boundaries. The maximum calculated containment accident pressure per 10 CFR 50 Appendix J (Pa) during the design basis accident would not create a substantial outleakage driving force and, in any case, tends to cause the relief valves to seat rather than lift. The systems feeding this line are ECCS and, due either to operating pressure or static head, outleakage would be prevented. Therefore, no Type C testing will be performed for this line. However, this line is exposed to the Pa test pressure during the Type A test.
(3) Containment Spray, X-48A, X-48B and RHR Spray, X-49A, X-49B These lines make use of an inboard containment isolation check valve and a CLOC for containment boundaries of each line. Additionally, a water leg seal exists against a system valve outside containment in each line. This seal 6.2.6-4 Containment Leakage Testing
WATTS BAR WBNP-112 prevents the outleakage of containment atmosphere. An inventory test is performed to ensure a 30-day seal water inventory at a pressure greater than 1.1 Pa, should one spray system shut down. The seal water inventory leakage rate test is performed in lieu of a Type C air leakage rate test of the containment isolation check valves.
(4) RHR Supply to Pumps, X-107 This line makes use of inboard containment isolation valves and a CLOC for containment boundaries. This penetration satisfies ANSI-N271-1976. In addition, an ASME Section XI water leakage test is performed to verify system integrity. Thus, no Type C test is required for this line.
Test connections and pressurizing means are provided to test isolation valves or barriers for leaktightness. Either air or nitrogen is used as the pressurizing medium, depending on the physical location and service of each line. Leak testing of individual valves and penetrations is accomplished by one of the following methods:
(1) Method 1, Pressure Decay The test volume initially shall be pressurized with air or nitrogen to a test pressure greater than the pressure under accident conditions, Pa. The final test pressure shall be greater than Pa. The pressure and temperature shall be recorded at the start and end of the test. The leakage rate shall be calculated from the following formula:
TV P 1 P 2 T stp L i = -------- ------ - ------ -----------
t T 1 T 2 P stp Where:
Li = Local leak rate, cfm TV = Test volume, ft3 P1 = Initial pressure, psia P2 = Final pressure, psia T1 = Initial temperature, °R T2 = Final temperature, °R Tstp = Standard atmospheric temperature, °R Pstp = Standard atmospheric pressure, psia Containment Leakage Testing 6.2.6-5
WATTS BAR WBNP-112 t = Test duration, min.
(2) Method 2, - Makeup Flow Rate The test volume shall be pressured and maintained to at least 15 psig using a pressure regulator to maintain test pressure. Makeup fluid flow to the test volume required to maintain test pressure shall be used as the leakage rate of the barrier under test.
The acceptance criteria for the Type C test are given in the Technical Specification which complies with Appendix J to 10 CFR 50, Option B.
6.2.6.3 Scheduling and Reporting of Periodic Tests Type A integrated containment leakage tests are performed prior to operation of the plant and subsequently in accordance with the Containment Leakage Rate Testing Program Type B and Type C leakage rate tests are performed in accordance with the Containment Leakage Rate Testing Program.
Test reports are made in accordance with 10 CFR 50 Appendix J, Option B.
References (1) Title 10, Code of Federal Regulations, Part 50, Appendix J, Option B, Primary Reactor Containment Leakage Testing for Water-Cooled Power Reactors - Performance-Based Requirements.
(2) Regulatory Guide 1.163, Performance-Based Containment Leak-Test Program, September 1995.
(3) NEI 94-01, Revision 0, Industry Guideline for Implementing Performance-Based Option of 10CFR Part 50, Appendix J.
6.2.6-6 Containment Leakage Testing
WATTS BAR WBNP-112 Table 6.2.6-1 Penetrations Subjected To Type B Testing (Page 1 of 3)
Penetration Description X-121E RCP No. 1 - Non-Div.
X-122E RCP No. 2 - Non-Div.
X-123E RCP No. 3 - Non-Div.
X-124E RCP No. 4 - Non-Div.
X-125E 480V Power - Non-Div.
X-126E 480V Power A X-127E 480V Power B X-128E 480V Power A X-129E 480V Power B X-130E Control - Non-Div.
X-131E 480V Power - Non-Div.
X-132E Control Rod Drive Power X-133E Control Rod Drive Power X-134E 480V Power A X-135E 480V Power A X-136E 480V Power B X-137E 480V Power B X-138E Low Level - Non-Div.
X-139E Process Instr. Protection X-140E Incore Instrumentation X-141E 480V Power A X-142E Incore Instrumentation X-143E NIS Channel III X-144E 480V Power - Non-Div.
X-145E Control Rod Pos. Detection X-146E Control Rod Drive Power X-147E Control A X-148E Process Inst. Control X-149E Low Level - Non-Div.
X-150E Annunciation and Communication X-151E NIS Channel IV X-152E 480V Power - Non-Div.
X-153E Low Level - Non-Div.
X-154E Process Inst. Control X-155E 480V Power - Non-Div.
X-156E Control B X-157E Annunciation X-158E Process Inst. Protection X-159E Process Inst. Control Containment Leakage Testing 6.2.6-7
WATTS BAR WBNP-112 Table 6.2.6-1 Penetrations Subjected To Type B Testing (Page 2 of 3)
Penetration Description X-160E Annunciation and Communication X-161E 480V Power - Non-Div.
X-163E NIS Channel I X-164E Control A X-165E Process Inst. Protection X-166E Control - Non-Div.
X-167E 480V Power - Non-Div.
X-168E Control - Non-Div.
X-169E Process Inst. Protection X-170E Process Inst. Control X-171E Control - Non-Div.
X-172E Control B X-173E Control - Non-Div.
X-174E NIS Channel II X-1 * (Resilient Seal)
X-2A * (Resilient Seal)
X-2B * (Resilient Seal)
X-3 * (Resilient Seal)
X-54 * (Resilient Seal)
X-79A * (Resilient Seal)
X-13A * (Bellows)
X-13B * (Bellows)
X-13C * (Bellows)
X-13D * (Bellows)
X-12A * (Bellows)
X-12B * (Bellows)
X-12C * (Bellows)
X-12D * (Bellows)
X-17 * (Bellows)
X-107 * (Bellows)
X-14A * (Bellows)
X-14B * (Bellows)
X-14C * (Bellows)
X-14D * (Bellows)
X-15 * (Bellows)
X-20A * (Bellows)
X-20B * (Bellows)
X-21 * (Bellows)
X-22 * (Bellows)
X-24 * (Bellows)
X-40D * (Resilient Seal)
X-79B * (Resilient Seal)
X-8A * (Bellows)
X-8B * (Bellows)
X-8C * (Bellows)
X-8D * (Bellows)
X-30 * (Bellows)
X-32 * (Bellows)
X-33 * (Bellows) 6.2.6-8 Containment Leakage Testing
WATTS BAR WBNP-112 Table 6.2.6-1 Penetrations Subjected To Type B Testing (Page 3 of 3)
Penetration Description X-45 * (Bellows)
X-46 * (Bellows)
X-47A * (Bellows)
X-47B * (Bellows)
X-81 * (Bellows)
X-108 * (Resilient Seal)
X-108 * (Bellows)
X-109 * (Resilient Seal)
X-109 * (Bellows)
X-36 * (Resilient Seal)
X-37 * (Resilient Seal)
X-117 * (Resilient Seal)
X-118 * (Resilient Seal)
- See Table 6.2.4-1 for Description.
Containment Leakage Testing 6.2.6-9
WATTS BAR WBNP-112 Table 6.2.6-2 Containment Isolation Valves Subjected to Type C Testing (Page 1 of 6)
Penetration No. Isolation Valve No. Description X-4 30-56(1) (2) 30-57 30-555 X-5 30-58(1) (2) 30-59 30-554 X-6 30-50(1) (2) 30-51 30-558 X-7 30-52(1) (2) 30-53 30-557 X-9A 30-7 (2) 30-8(1)30-563 X-9B 30-9 (2) 30-10(1)30-562 X-10A 30-14 (2) 30-15(1)30-561 X-10B 30-16 (2) 30-17(1)30-560 (2)
X-11 30-19 30-20(1)30-559 (2)
X-15 62-72 62-73 62-74 62-76 62-77 62-662(1)
X-25A 43-11 (2) 43-12 X-25D 43-2 (2) 43-3 6.2.6-10 Containment Leakage Testing
WATTS BAR WBNP-112 Table 6.2.6-2 Containment Isolation Valves Subjected to Type C Testing (Page 2 of 6)
Penetration No. Isolation Valve No. Description (2)
X-26B 52-500 52-504 (2)
X-26A 52-501 52-505 (2)
X-29 70-89 70-92 70-698 (2)
X-30 63-71 63-84 63-23 63-28 (2)
X-31 26-243 26-1296 (2)
X-34 32-111 32-338 32-343 (2)
X-35 70-85 70-703(1)
(2)
X-39A 63-64 63-868 (2)
X-39B 68-305 68-849 (2)
X-41 77-127 77-128 77-2875 (2)
X-42 81-12 81-502 (2)
X-44 62-61 62-63 62-639 (2)
X-45 77-18 77-19 77-20 (2)
X-46 77-9 77-10 84-530 (2)
X-47A 61-191 61-192 61-533 Containment Leakage Testing 6.2.6-11
WATTS BAR WBNP-112 Table 6.2.6-2 Containment Isolation Valves Subjected to Type C Testing (Page 3 of 6)
Penetration No. Isolation Valve No. Description (2)
X-47B 61-193 61-194 61-680 (2)
X-50A 70-87 70-90 70-687 (2)
X-50B 70-679 70-134 (2)
X-52 70-140 70-100 70-790 (2)
X-53 70-143 (2)
X-56A 67-107 67-113 67-1054D (2)
X-57A 67-111 67-112 67-575D (2)
X-58A 67-83 67-89 67-1054A (2)
X-59A 67-87 67-88 67-575A (2)
X-60A 67-99 67-105 67-1054B (2)
X-61A 67-103 67-104 67-575B (2)
X-62A 67-91 67-97 67-1054C (2)
X-63A 67-95 67-96 67-575C (2)
X-64 31-305 31-306 31-3421 6.2.6-12 Containment Leakage Testing
WATTS BAR WBNP-112 Table 6.2.6-2 Containment Isolation Valves Subjected to Type C Testing (Page 4 of 6)
Penetration No. Isolation Valve No. Description (2)
X-65 31-309 31-308 31-3407 (2)
X-66 31-326 31-327 31-3392 (2)
X-67 31-330 31-329 31-3378 (2)
X-68 67-141 67-580D (2)
X-69 67-130 67-580A (2)
X-70 67-139 67-297 67-585B (2)
X-71 67-134 67-296 67-585C (2)
X-72 67-142 67-298 67-585D (2)
X-73 67-131 67-295 67-585A (2)
X-74 67-138 67-580B (2)
X-75 67-133 67-580C (2)
X-76 33-713 (Unit 1)33-714 (Unit 1)33-732 (Unit 2)33-733 (Unit 2)
(2)
X-77 59-522 59-698 (2)
X-78 26-240 26-1260 Containment Leakage Testing 6.2.6-13
WATTS BAR WBNP-112 Table 6.2.6-2 Containment Isolation Valves Subjected to Type C Testing (Page 5 of 6)
Penetration No. Isolation Valve No. Description (2)
X-80 30-37 30-40 30-556 (2)
X-81 77-16 77-17 (2)
X-82 78-560 78-561 (2)
X-83 78-557 78-558 (2)
X-84A 68-307 68-308 (2)
X-85B 43-22 43-23 (2)
X-90 32-103 32-318 32-323 (2)
X-91 32-81 32-328 32-333 (2)
X-93 43-34 43-35 (2)
X-94B 90-110 90-111 (2)
X-94C 90-107 90-108 90-109 (2)
X-95B 90-116 90-117 (2)
X-95C 90-113 90-114 90-115 (2)
X-96A 52-506 52-502 (2)
X-96B 52-507 52-503 (2)
X-99 43-202 43-434 6.2.6-14 Containment Leakage Testing
WATTS BAR WBNP-112 Table 6.2.6-2 Containment Isolation Valves Subjected to Type C Testing (Page 6 of 6)
Penetration No. Isolation Valve No. Description (2)
X-100 43-201 43-433 (2)
X-114 61-110 61-122 61-745 (2)
X-115 61-96 61-97 61-692 Notes:
(1) These isolation valves are leakage rate tested in the reverse direction. This is acceptable since the results are equivalent or more conservative.
(2) See Table 6.2.4-1 for Description.
Containment Leakage Testing 6.2.6-15
WATTS BAR WBNP-112 Table 6.2.6-3 Valves Exempted From Type C Leak Testing (Page 1 of 6)
Penetration No. Valve No. System Justification X-8A FCV 3-236 Note 12 Note 1 LCV 3-164 Note 1 LCV 3-174 Note 1 LCV 3-164A Note 1 X-8B FCV 3-239 Note 12 Note 1 X-8C FCV 3-242 Note 12 Note 1 X-8D FCV 3-245 Note 12 Note 1 LCV 3-171 Note 1 LCV 3-175 Note 1 LCV 3-171A Note 1 X-12A FCV 3-33 Note 12 Note 1 X-12B FCV 3-47 Note 12 Note 1 X-12C FCV 3-87 Note 12 Note 1 X-12D FCV 3-100 Note 12 Note 1 X-13A FCV 1-4 Note 12 Note 1 FCV 1-147 Note 1 FCV 1-15 Note 1 DRV 1-536 Note 1 PCV 1-5 Note 1 SFV 1-522 Note 1 SFV 1-523 Note 1 SFV 1-524 Note 1 SFV 1-525 Note 1 SFV 1-526 Note 1 X-13B FCV 1-11 Note 12 Note 1 FCV 1-148 Note 1 PCV 1-12 Note 1 DRV 1-534 Note 1 SFV 1-517 Note 1 SFV 1-518 Note 1 SFV 1-519 Note 1 SFV 1-520 Note 1 SFV 1-521 Note 1 6.2.6-16 Containment Leakage Testing
WATTS BAR WBNP-112 Table 6.2.6-3 Valves Exempted From Type C Leak Testing (Page 2 of 6)
Penetration No. Valve No. System Justification X-13C FCV 1-22 Note 12 Note 1 PCV 1-23 Note 1 FCV 1-149 Note 1 DRV 1-532 Note 1 SFV 1-512 Note 1 SFV 1-513 Note 1 SFV 1-514 Note 1 SFV 1-515 Note 1 SFV 1-516 Note 1 X-13D FCV 1-29 Note 12 Note 1 FCV 1-150 Note 1 PCV 1-30 Note 1 DRV 1-538 Note 1 FCV 1-16 Note 1 SFV 1-527 Note 1 SFV 1-528 Note 1 SFV 1-529 Note 1 FCV 1-530 Note 1 SFV 1-531 Note 1 X-14A FCV 1-14 Note 12 Note 1 X-14B FCV 1-32 Note 12 Note 1 X-14C FCV 1-25 Note 12 Note 1 X-14D FCV 1-7 Note 12 Note 1 X-16 62-543* Note 12 Note 3 X-17 63-640* Note 12 Note 2 63-643* Note 2 FCV 63-158 Note 2 X-19A FCV 63-72 Note 12 Note 5 FCV 72-44 Note 5 X-19B FCV 63-73 Note 12 Note 5 FCV 72-45 Note 5 X-20A FCV 63-112 Note 12 Note 2 63-633* Note 2 63-635* Note 2 X-20B FCV 63-111 Note 12 Note 2 63-632* Note 2 63-634* Note 2 X-21 FCV 63-167 Note 12 Note 6 63-547* Note 6 63-549* Note 6 Containment Leakage Testing 6.2.6-17
WATTS BAR WBNP-112 Table 6.2.6-3 Valves Exempted From Type C Leak Testing (Page 3 of 6)
Penetration No. Valve No. System Justification X-22 FCV 63-174 Note 12 Note 7 63-581* Note 7 X-24 68-559* Note 12 Note 8 X-27A FCV 43-55 Note 12 Note 1 X-27B FCV 43-58 Note 12 Note 1 X-27C FCV 43-61 Note 12 Note 1 X-27D FCV 43-64 Note 12 Note 1 X-32 FCV 63-21 Note 12 Note 6 63-543* Note 6 63-545* Note 6 6.2.6-18 Containment Leakage Testing
WATTS BAR WBNP-112 Table 6.2.6-3 Valves Exempted From Type C Leak Testing (Page 4 of 6)
Penetration No. Valve No. System Justification X-33 FCV 63-121 Note 12 Note 6 63-551 Note 6 63-553 Note 6 63-555 Note 6 63-557 Note 6 X-40A LCV 3-156 Note 12 Note 1 LCV 3-173 Note 1 LCV 3-156A Note 1 X-40B LCV 3-148 Note 12 Note 1 LCV 3-172 Note 1 LCV 3-148A Note 1 X-43A 62-562* Note 12 Note 9 X-43B 62-561* Note 12 Note 9 X-43C 62-563* Note 12 Note 9 X-43D 62-560* Note 12 Note 9 X-48A 72-548* Note 12 Note 10 X-48B 72-549* Note 12 Note 10 X-49A 72-562* Note 12 Note 10 X-49B 72-563* Note 12 Note 10 X-107 FCV 74-2 Note 12 Note 4 FCV 74-8 Note 4 RFV 74-505 Note 4 FCV 63-185 Note 4
- Check Valve Containment Leakage Testing 6.2.6-19
WATTS BAR WBNP-112 Table 6.2.6-3 Valves Exempted From Type C Leak Testing (Page 5 of 6)
Note 1. This penetration is directly connected to the secondary side of the steam generator.
The main steam, feedwater, and steam generator blowdown lines of PWR containments are not required to be tested (see definition of Type C test in 10 CFR 50, Appendix J).
These lines are assumed not to rupture as a result of an accident (missile Protected).
Any leakage through these lines would be identified during operation by the leakage detection program. In addition, during a design basis accident, the secondary side would be at a higher pressure than the containment atmosphere, thus preventing outleakage from containment. The integrity of the inside piping is also verified during the Type A test.
Note 2. This penetration uses inboard containment isolation valves and a CLOC for containment boundaries. Type C testing for this penetration is not required since a continuous water seal will be provided at a pressure greater than 1.1 Pa and a guaranteed 30-day water inventory. Testing will be performed in accordance with ASME XI.
Note 3. This penetration uses an inboard check valve and a closed loop outside containment (CLOC) as the means of containment isolation. Type C testing for this path is not required due to the presence of a 1.1 Pa pressure and a 30-day inventory criteria. A positive pressure preventing air outleakage is assured by the pressure applied against FCV-62-90 and FCV-62-91 (both of which receive a phase A signal) by the high-head SI pumps. Water testing for piping integrity is performed in accordance with ASME XI.
Note 4. This line makes use of inboard containment isolation valves and a CLOC for containment boundaries. This penetration satisfies ANSI-N271-1976. In addition, an ASME Section XI water leakage test will be performed to verify system integrity.
Note 5. This line makes use of a containment isolation valve located outside of containment and a CLOC for containment isolation boundaries. During a design basis accident, this line would be submerged under water which would preclude air outleakage. In addition, these valves are exposed to Pa during each Type A test.
Note 6. This line makes use of inboard containment isolation valves and a CLOC for containment boundaries. These lines are postulated to be inservice post-accident and when not in use, the pumps maintain a pressure seal greater than 1.1 Pa.
6.2.6-20 Containment Leakage Testing
WATTS BAR WBNP-112 Table 6.2.6-3 Valves Exempted From Type C Leak Testing (Page 6 of 6)
Note 7. This line makes use of inboard containment isolation valves and a CLOC for containment boundaries. Type C testing is not required for the same reasons as X-21 and X-32 as stated in Note 6. Water seal is provided by the high-head pumps.
Note 8. This line uses an inboard containment isolation valve and a CLOC for containment boundaries. Pa during the design basis accident would not create a substantial outleakage driving force and, in any case, tend to cause the relief valves in the CLOC to seat rather than lift. The systems feeding this line are ECCS and, due either to operating pressure or static head outleakage would be prevented. This line is exposed to the Pa test pressure during the Type A test.
Note 9. This line makes use of an inboard containment isolation valve and a CLOC for containment boundaries. Type C testing is not required for the same reason as given for X-16 in Note 3.
Note 10. This line makes use of an inboard containment isolation valve and a CLOC for containment boundaries. An inventory test is performed to ensure a 30-day inventory at a pressure greater than 1.1 Pa exists, should one spray system shut down. This will prevent outleakage of containment atmosphere.
Note 11. Not used.
Note 12. See Table 6.2.4-1 for System information.
Containment Leakage Testing 6.2.6-21
WATTS BAR WBNP-112 Table 6.2.6-4 Containment Vessel Pressure And Leak Test Reactor Building Containment Penetration Status (Page 1 of 8)
Penetration Description Status A. PENETRATION STATUS DURING TEST PERFORMANCE X-1 (see Note 4.) Closed X-2A (see Note 4.) Closed X-2B (see Note 4.) Closed X-3 (see Note 4.) Closed X-4 (see Note 4.) Vented X-5 (see Note 4.) Vented X-6 (see Note 4.) Vented X-7 (see Note 4.) Vented X-8 (see Note 4.) Vented (see Note 1)
X-8A (see Note 4.) Normal Lineup X-8B (see Note 4.) Normal Lineup X-8C (see Note 4.) Normal Lineup X-8D (see Note 4.) Normal Lineup X-9A (see Note 4.) Vented X-9B (see Note 4.) Vented X-10A (see Note 4.) Vented X-10B (see Note 4.) Vented X-11 (see Note 4.) Vented X-12A (see Note 4.) Normal Lineup X-12B (see Note 4.) Normal Lineup X-12C (see Note 4.) Normal Lineup X-12D (see Note 4.) Normal Lineup X-13A (see Note 4.) Normal Lineup X-13B (see Note 4.) Normal Lineup X-13C (see Note 4.) Normal Lineup X-13D (see Note 4.) Normal Lineup X-14A (see Note 4.) Normal Lineup X-14B (see Note 4.) Normal Lineup X-14C (see Note 4.) Normal Lineup X-14D (see Note 4.) Normal Lineup X-15 (see Note 4.) See Note 3 X-16 (see Note 4.) Normal Lineup X-17 (see Note 4.) Normal Lineup X-18 (see Note 4.) Vented (see Note 1)
X-19A (see Note 4.) Normal Lineup X-19B (see Note 4.) Normal Lineup X-20A (see Note 4.) Normal Lineup 6.2.6-22 Containment Leakage Testing
WATTS BAR WBNP-112 Table 6.2.6-4 Containment Vessel Pressure And Leak Test Reactor Building Containment Penetration Status (Page 2 of 8)
Penetration Description Status X-20B (see Note 4.) Normal Lineup X-21 (see Note 4.) Normal Lineup X-22 (see Note 4.) Normal Lineup X-23 (see Note 4.) Vented (See Note 1)
X-24 (see Note 4.) Vented X-25A (see Note 4.) See Note 3 X-25B (see Note 4.) Vented (See Note 1)
X-25C (see Note 4.) Vented (See Note 1)
X-25D (see Note 4.) See Note 3 X-26A (see Note 4.) In Use (see Note 2)
X-26B (see Note 4.) In Use (see Note 2)
X-26C (see Note 4.) Normal Lineup X-27A (see Note 4.) Normal Lineup X-27B (see Note 4.) Normal Lineup X-27C (see Note 4.) Normal Lineup X-27D (see Note 4.) Normal Lineup X-28 (see Note 4.) Vented (See Note 1)
X-29 (see Note 4.) See Note 3 X-30 (see Note 4.) See Note 3 X-31 (see Note 4.) See Note 3 X-32 (see Note 4.) Normal Lineup X-33 (see Note 4.) Normal Lineup X-34 (see Note 4.) Vented X-35 (see Note 4.) See Note 3 X-36 (see Note 4.) Vented (see Note 1)
X-37 (see Note 4.) Vented (see Note 1)
X-38 (see Note 4.) Vented (see Note 1)
X-39A (see Note 4.) Vented X-39B (see Note 4.) Vented X-39C (see Note 4.) Vented (see Note 1)
X-39D (see Note 4.) Vented (see Note 1)
X-40A (see Note 4.) Normal Lineup X-40B (see Note 4.) Normal Lineup X-40C (see Note 4.) Vented (see Note 1)
X-40D (see Note 4.) Vented X-41 (see Note 4.) See Note 3 X-42 (see Note 4.) See Note 3 X-43A (see Note 4.) Normal Lineup X-43B (see Note 4.) Normal Lineup X-43C (see Note 4.) Normal Lineup X-43D (see Note 4.) Normal Lineup X-44 (see Note 4.) See Note 3 X-45 (see Note 4.) Vented X-46 (see Note 4.) See Note 3 Containment Leakage Testing 6.2.6-23
WATTS BAR WBNP-112 Table 6.2.6-4 Containment Vessel Pressure And Leak Test Reactor Building Containment Penetration Status (Page 3 of 8)
Penetration Description Status X-47A (see Note 4.) In Use X-47B (see Note 4.) In Use X-48A (see Note 4.) Normal Lineup X-48B (see Note 4.) Normal Lineup X-49A (see Note 4.) Normal Lineup X-49B (see Note 4.) Normal Lineup X-50A (see Note 4.) See Note 3 X-50B (see Note 4.) See Note 3 X-51 (see Note 4.) Vented (see Note 1)
X-52 (see Note 4.) See Note 3 X-53 (see Note 4.) See Note 3 X-54 (see Note 4.) In Use X-55 (see Note 4.) Vented (see Note 1)
X-56A (see Note 4.) See Note 3 X-56B (see Note 4.) Vented (see Note 1)
X-57A (see Note 4.) See Note 3 X-57B (see Note 4.) Normal Lineup X-58A (see Note 4.) See Note 3 X-58B (see Note 4.) Normal Lineup X-59A (see Note 4.) See Note 3 X-59B (see Note 4.) Vented (see Note 1)
X-60A (see Note 4.) See Note 3 X-60B (see Note 4.) Normal Lineup X-61A (see Note 4.) See Note 3 X-61B (see Note 4.) Vented (see Note 1)
X-62A (see Note 4.) See Note 3 X-62B (see Note 4.) Vented (see Note 1)
X-63A (see Note 4.) See Note 3 X-63B (see Note 4.) Vented (see Note 1)
X-64 (see Note 4.) See Note 3 X-65 (see Note 4.) See Note 3 X-66 (see Note 4.) See Note 3 X-67 (see Note 4.) See Note 3 X-68 (see Note 4.) See Note 3 X-69 (see Note 4.) See Note 3 X-70 (see Note 4.) See Note 3 X-71 (see Note 4.) See Note 3 X-72 (see Note 4.) See Note 3 X-73 (see Note 4.) See Note 3 X-74 (see Note 4.) See Note 3 X-75 (see Note 4.) See Note 3 X-76 (see Note 4.) Vented X-77 (see Note 4.) See Note 3 6.2.6-24 Containment Leakage Testing
WATTS BAR WBNP-112 Table 6.2.6-4 Containment Vessel Pressure And Leak Test Reactor Building Containment Penetration Status (Page 4 of 8)
Penetration Description Status X-78 (see Note 4.) See Note 3 X-79A (see Note 4.) Vented X-79B (see Note 4.) Vented X-80 (see Note 4.) Vented X-81 (see Note 4.) See Note 3 X-82 (see Note 4.) See Note 3 X-83 (see Note 4.) See Note 3 X-84A (see Note 4.) See Note 3 X-84B (see Note 4.) Normal Lineup X-84C (see Note 4.) Normal Lineup X-84D (see Note 4.) Normal Lineup X-85A (see Note 4.) Vented (see Note 1)
X-85B (see Note 4.) See Note 3 X-85C (see Note 4.) Vented (see Note 1)
X-85D (see Note 4.) Vented (see Note 1)
X-86A (see Note 4.) Vented (see Note 1)
X-86B (see Note 4.) Vented (see Note 1)
X-86C (see Note 4.) Vented (see Note 1)
X-86D (see Note 4.) Vented (see Note 1)
X-87A (see Note 4.) Vented (see Note 1)
X-87B (see Note 4.) Normal Lineup X-87C (see Note 4.) Normal Lineup X-87D (see Note 4.) Normal Lineup X-88 (see Note 4.) Vented (see Note 1)
X-89 (see Note 4.) Vented (see Note 1)
X-90 (see Note 4.) Vented X-91 (see Note 4.) Vented X-92A (see Note 4.) Vented (see Note 1)
X-92B (see Note 4.) Vented (see Note 1)
X-92C (see Note 4.) Vented (see Note 1)
X-92D (see Note 4.) Vented (see Note 1)
X-93 (see Note 4.) See Note 3 X-94A (see Note 4.) Vented (see Note 1)
X-94B (see Note 4.) Vented X-94C (see Note 4.) Vented X-95A (see Note 4.) Vented (see Note 1)
X-95B (see Note 4.) Vented X-95C (see Note 4.) Vented X-96A (see Note 4.) In Use (see Note 2)
X-96B (see Note 4.) In Use (see Note 2)
X-96C (see Note 4.) Vented (see Note 1)
X-97 (see Note 4.) Vented (see Note 1)
X-98 (see Note 4.) Vented (see Note 1)
Containment Leakage Testing 6.2.6-25
WATTS BAR WBNP-112 Table 6.2.6-4 Containment Vessel Pressure And Leak Test Reactor Building Containment Penetration Status (Page 5 of 8)
Penetration Description Status X-99 (see Note 4.) Vented X-100 (see Note 4.) Vented X-101 (see Note 4.) Vented (see Note 1)
X-102 (see Note 4.) Normal Lineup X-103 (see Note 4.) Vented (see Note 1)
X-104 (see Note 4.) Vented (see Note 1)
X-105 (see Note 4.) Vented (see Note 1)
X-106 (see Note 4.) Vented (see Note 1)
X-107 (see Note 4.) Normal Lineup X-108 (see Note 4.) Vented (see Note 1)
X-109 (see Note 4.) Vented (see Note 1)
X-110 (see Note 4.) Vented (see Note 1)
X-111 (see Note 4.) Vented (see Note 1)
X-112 (see Note 4.) Vented (see Note 1)
X-113 (see Note 4.) Vented (see Note 1)
X-114 (see Note 4.) In Use X-115 (see Note 4.) In Use X-116 (see Note 4.) Vented (see Note 1)
X-117 (see Note 4.) Vented (see Note 1)
X-118 (see Note 4.) In Use X-119 (see Note 4.) Vented (see Note 1)
X-120 (see Note 4.) Vented (see Note 1)
X-121E Electrical Penetration Vented (see Note 1)
X-122E Electrical Penetration Vented (see Note 1)
X-123E Electrical Penetration Vented (see Note 1)
X-124E Electrical Penetration Vented (see Note 1)
X-125E Electrical Penetration Vented (see Note 1)
X-126E Electrical Penetration Vented (see Note 1)
X-127E Electrical Penetration Vented (see Note 1)
X-128E Electrical Penetration Vented (see Note 1)
X-129E Electrical Penetration Vented (see Note 1)
X-130E Electrical Penetration Vented (see Note 1)
X-131E Electrical Penetration Vented (see Note 1)
X-132E Electrical Penetration Vented (see Note 1)
X-133E Electrical Penetration Vented (see Note 1)
X-134E Electrical Penetration Vented (see Note 1)
X-135E Electrical Penetration Vented (see Note 1)
X-136E Electrical Penetration Vented (see Note 1)
X-137E Electrical Penetration Vented (see Note 1)
X-138E Electrical Penetration Vented (see Note 1)
X-139E Electrical Penetration Vented (see Note 1)
X-140E Electrical Penetration Vented (see Note 1)
X-141E Electrical Penetration Vented (see Note 1)
X-142E Electrical Penetration Vented (see Note 1) 6.2.6-26 Containment Leakage Testing
WATTS BAR WBNP-112 Table 6.2.6-4 Containment Vessel Pressure And Leak Test Reactor Building Containment Penetration Status (Page 6 of 8)
Penetration Description Status X-143E Electrical Penetration Vented (see Note 1)
X-144E Electrical Penetration Vented (see Note 1)
X-145E Electrical Penetration Vented (see Note 1)
X-146E Electrical Penetration Vented (see Note 1)
X-147E Electrical Penetration Vented (see Note 1)
X-148E Electrical Penetration Vented (see Note 1)
X-149E Electrical Penetration Vented (see Note 1)
X-150E Electrical Penetration Vented (see Note 1)
X-151E Electrical Penetration Vented (see Note 1)
X-152E Electrical Penetration Vented (see Note 1)
X-153E Electrical Penetration Vented (see Note 1)
X-154E Electrical Penetration Vented (see Note 1)
X-155E Electrical Penetration Vented (see Note 1)
X-156E Electrical Penetration Vented (see Note 1)
X-157E Electrical Penetration Vented (see Note 1)
X-158E Electrical Penetration Vented (see Note 1)
X-159E Electrical Penetration Vented (see Note 1)
X-160E Electrical Penetration Vented (see Note 1)
X-161E Electrical Penetration Vented (see Note 1)
X-162E Seal Welded Spare Vented (see Note 1)
X-163E Electrical Penetration Vented (see Note 1)
X-164E Electrical Penetration Vented (see Note 1)
X-165E Electrical Penetration Vented (see Note 1)
X-166E Electrical Penetration Vented (see Note 1)
X-167E Electrical Penetration Vented (see Note 1)
X-168E Electrical Penetration Vented (see Note 1)
X-169E Electrical Penetration Vented (see Note 1)
X-170E Electrical Penetration Vented (see Note 1)
X-171E Electrical Penetration Vented (see Note 1)
X-172E Electrical Penetration Vented (see Note 1)
X-173E Electrical Penetration Vented (see Note 1)
X-174E Electrical Penetration Vented (see Note 1)
Containment Leakage Testing 6.2.6-27
WATTS BAR WBNP-112 Table 6.2.6-4 Containment Vessel Pressure And Leak Test Reactor Building Containment Penetration Status (Page 7 of 8)
Penetration Description Status B. TESTABLE PENETRATIONS REQUIRED TO BE INSERVICE DURING TEST PERFORMANCE X-20A (see Note 4) Residual heat removal system required X-20B (see Note 4) inservice to remove decay heat from fuel X-26A (see Note 4) Isolation valves required to be open to X-26B monitor containment pressure (see Note 2)
X-47A (see Note 4) Glycol cooling supply to air handling units in ice condenser required to ensure ice condition is maintained X-47B (see Note 4) Glycol cooling return from air handling units in ice condenser required to ensure ice condition is maintained X-54 (see Note 4) Used as pressurization point for air compressors X-96A (see Note 4) Isolation valves required to be open to X-96B monitor containment pressure (see Note 2)
X-107 (see Note 4) Residual heat removal system required inservice to remove decay heat from fuel X-114 (see Note 4) Glycol return line from floor cooling coils required to ensure ice condition is maintained X-115 (see Note 4) Glycol supply line to floor cooling coils required to ensure ice condition is maintained 6.2.6-28 Containment Leakage Testing
WATTS BAR WBNP-112 Table 6.2.6-4 Containment Vessel Pressure And Leak Test Reactor Building Containment Penetration Status (Page 8 of 8)
Penetration Description Status X-118 (See Note 4) Used as source for verification flow and post-test depressurization; opened during DBF event to drain water from annulus to Reactor Building floor and equipment drain sump Notes:
- 1. These penetrations are closed. Venting is provided by the design of the penetration such that any leakage is detectable by the integrated leak rate test.
- 2. These penetrations are designed to facilitate ILRT performance. It may not be necessary to utilize all of the penetrations. If not in use, the penetration is vented.
- 3. These penetrations may remain water filled and/or unvented to facilitate planning and scheduling or for ALARA consideration provided they have been Type B or C tested within the previous 24 months.
- 4. See Table 6.2.4-1 for Description.
Containment Leakage Testing 6.2.6-29
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