ML19343A805
| ML19343A805 | |
| Person / Time | |
|---|---|
| Site: | McGuire, Mcguire  |
| Issue date: | 11/17/1980 |
| From: | DUKE POWER CO. |
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| Shared Package | |
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| References | |
| NUDOCS 8011210500 | |
| Download: ML19343A805 (400) | |
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-O TaiS oocuMENT CONTAINS P00R QUALITY PAGES DUKE POWER C0liPANY l
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AN ANALYSIS OF HYDROGEN CONTROL MEASURES .l AT MCGUIRE NUCLEAR STATION VOLUME 1 l 1
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- 1. INTRODUCTION 1.1 Duke Power's Inyclument in Hydrogen Control Studies
1.2 Background
1.3 McGuire Nuclear Station and Design Basis Hydrogen Control 1.4 Hydrogen Control Efforts Beyond the Design Basis for McGuire Nuclear Station 1-1
1.1 Duke Power's Involvement in Hydrogen Control Studies The accident which occurred at Three Mile Island (TMI) VAit 2 has prompted a reevaluation of the hydrogen control measures at light water cooled nuclear power plants. Duke Power has participated in this reevaluation since January, 1980, and has established a task force to exam!ne hydrogen control measures at McGuire Nuclear Station. This task force has performed work specifically related to McGuire, reviewed Tennessee Valley Authority (TVA) actions regarding the Sequoyah Nuclear Plant, and monitored NRC and industry activities relating to hydrogen control. In addition a joirt effort with TVA and American Electric Power (AEP) was instituted in June, 1980 to study hydrogen control measures as they pertain to nuclear power plants with ice condenser containments. Duke Power, TVA, and AEP are currently sponsoring an experimental program to further determine the characteristics of a hydrogen burn in a nuclear power plant containment building and a feasibility study of a Halon suppression system for hydrogen mitigation. Many other concepts for hydrogen mitigation are also being evaulated.
< 1.2 Background Light water cooled nuclear power plants include safety features to prevent accidents which could lead to the generation of excessive amounts of hydrogen by the reactor core and to mitigate the effects of such accidents should they occur. The design criteria for these safety feutures have been established by the Nuclear Regulatory Commission (NRC) and are set forth in 10CFR 550.44, Standards for combustible gas control system in light water cooled power reactors, and in General Design Criteria 50 in Appendix A to 10CFR Part 50.
I Section 50.44 requires a licensee or license applicant to show that, during I the time immediately fol .s 'ing a postulated loss-of-coolant accident (LOCA) 1-2
but before effective operation of the combustible gas control system, either:
(1) an uncontrolled hydrogen-oxygen recombination will not take place in the containment, or (2) the plant can withstand the consequences of uncontrolled hydrogen-oxygen recombination without loss of safety. If neither of these conditions can be shown, the conthinment must be provided with an inerted atmosphere or an oxygen deficient condition in order to provide protection against hydrogen burning and explosions during this time.
4 Section 50.44 give credit to performance of the emergency core cooling system (ECSS) by specifying that the amount of hydrogen assumed to be contributed by the metal-water reaction snall be either five times the total amount of hydrogen calculated in dennnstrating compliance with the ECCS ccceptance criteria (550.46, Acceptance Criteria for Emergency Core Cooling Systems for Light Water Nuclear Power Reactors) or an amount related to a specific depth of fuel clad reacted (approximately one percent of tne fuel clad) whichever amount is greater.
However, the accident which occurred at TMI Unit 2 resulted in hydrogen genera-tion well in excess of the amounts required to be considered for design purposes by 10CFR 550.44. Consequently, the NRC has taken several actions designed to prevent the reoccurrence o" a TMI-type accident, that is a small break LOCA accompanied by.the premature termination of the ECCS. In addition, the NRC has begun a reevaluation of its hydrogen control regulations. This reevalua-tion includes NRC documents SECY 80-107, 80-107A, 80-107B, Proposed Interim Hydrogen Control Requirements for Small Containments; a proposed rule, Interim Requirements Related to Hydrogen Control and Certain Degraded Core Considera-tions; and a proposed rulemaking proceeding, Consideration of Degraded or Melted Cores .in Safety Regulation.
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1.3 McGuire Nuclear Station and Design Basis Hydrogen Control McGuire Nuclear Station has been designed and constructed in compliance with NRC regulations. The McGuire ECCS meets 10CFR 550.46, 10CFR 550 Appendix A, Criterion 35, and Appendix ). The operation of the ECCS as designed, therefcre, precludes the generation of uydrogen in excess of the limits specified in 10CFR 550.44. The NRC Staff concurred in this position in the McGuire Nuclear Station Safety Evaluation Report Supplement 2, March,1979, pp 6-4, 6-7, 6-8.
With respect to actual operation of the McGuire ECCS in a TMI-type accident, such is assured by actions undertaken by Duke Power, the NRC, and other organizations in the nuclear industry in response to the accident at TMI Unit 2.
These actions included (1) changes in the McGuire administrative procedures, (2) hardware modifications of the plant, (3) increased and more comprehensive training programs, (4) additional and better informed control room personnel, and (5) additional support from organizations such as the Institute for Nuclear Power Operations and the Nuclear Safety Analysis Center. Further description of actions implemented at McGuire Nuclear Station in response to the accident at TMI Unit 2 is provided in the document, " Duke Power Company, McGuire Nuclear Station, Response to TMI Concerns." These actions in conjunc-tion with the existing McGuire design and Duke Power Company experience in operating nuclear power plants assure that in the unlikely event of a THI-type accident at McGuire hydrogen would not be generated in excess of concentration limits set forth in 10CFR 550.44.
1.4 Hydrogen Control Efforts Beyond the Design Basis for McGuire Nuclear Station This report provides the results of some of Duke Power Company's efforts in the area of hydrogen control beyond the design basis for McGuire Nuclear Station. Chapter 2 describes the pressures and temperatures which would 1-4
result from the burning of hydrogen generated by a TMf-type accident at McGuire.
This analysis was performed by Westinghouse /0ffshore Power Systems (W/0PS) using the CLASIX computer code. CLASIX is a multi-compartment containment code which calculates pressure and temperature response for the individual compartments while monitoring the distribution of oxygen, nitrogen, steam, and hydrogen.
The only passive heat sink modeled by CLASIX is the ice bed. The CLASIX analysis demonstrates that when hydrogen generated by a THI-type accident burns in an ice condenser containment at a concentration of 8-to-10 percent in air the resultant pressures range from approximately 15 psig (30 psia) (full safeguards) tc approximately 60 psig (75 psia) (minimum safeguards).
Chapter 3 describes a hydrogen mitigation system which Duke Power is installing in the Unit I containment of McGuire Nuclear Station. This system employs distributed hydrogen ignition sources located throughout the containment build-ing. The decision to install this hydrogen iattigation system was based on the determination that this system would provide an additional assurance of safety in the event of excessive hydrogen generation resulting from an accident beyond the design basis for McGuire Nuclear Station. This decision was not based on a i determination that this system was necessary for the safe operation of the plant.
Chapter 4 describes a detailed analysis of the structural integrity of the McGuire containment. This analysis was performed by Duke power and revealed that the ultimate capacity of the McGuire containment is approximately 67.5 psig (82.5 psia). An independent structural analysis performed by W/0PS revealed an ultimate capacity of approximately 68 psig (83 psia). These analyses demonstrate that if the hydrogen burn which occurred at TMI Unit 2 had occurred at McGuire the resultant pressure (assuming uniform mixing and adiabatic burning) would not have failed the McGuire containment. .Thev also demonstrate that the McGuire con-tainment can withstand the range of hydrogen burns considered in the CLASIX analysis.
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Duke Power is engaged in other activities relating to hydrogen control measures for nuclear power plants. Chief among these is an experimental program to further determine the characteristics of a hydrogen burn in a nuclear power plant containment building. Included in these experiments are tests of the ignition sources used at both McGuire Nuclear Station and Sequoyah Nuclear Plant. This experimental program is being conducted by Fenwall, Incorporated in conjunction with Westinghousa and Combustion and Explosives Research Company and is being sponsored by Duke Power, TVA, and AEP. A future report will document the results of this program.
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,. 2. CONTAINMENT RESPONSE TO HYDR 0 GEN TRANSIENTS 2.1 Summary of Analyses of Ice Condenser Containment Response to Hydrogen Burn Transients 2.1.1 Introduction 2.1.2 CLASIX Base Case Analysis 2.1.3 CLASIX Sensitivity Studies 2.1.4 Summary and Conclusions 2.2 ,ummary of Analyses of McGuire Containment Response to Hydrogen Burn Transients 2.2.1 Introduction 2.2.2 McGuire Plant Parameters 2.2.3 McGuir. Analyses 2.2.4 McGuire Results 2.3 CLASIX Program Description 2.3.1 Introduction 2.3.2 Analytical Model 2.3.3 Program Description 2.3.4 Summary 2.4 Verification of CLASIX 2.4.1 Introduction 2.4.2 TMD Comparisons 2.4.3 C0C0 CLASS 9 Comparisons 2.4.4 Discussion of Results 2.4.5 Other Verification 2.4.6 Future Work 2.4.7 Conclusion 2-1
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2.1 Summary of Analyses of Ice Condenser Containment Resoonse to Hydrogen Burn Transient 2.1.1 Introduction A series of analyses have been performed to study. fce condenser containment response to hydrogen burn transients for an accident sequence similar to the TMI-2 accident. .The particular sequence studied is that designated as S2D in WASH-1400. This is a small break loss of coolant accident (LOCA) accom-panied by the failure of emergency core cooling injection.
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The S20 transient may be divided into three phases. The first phase is the j period fre n accident initiation to the beginning of hydrogen generation.
This peritd is similar to the small break LOCA transient. Existing calcula-tional techniques such as tl.s Westinghouse Long Term Ice Condenser Contain-ment Code (LOTIC) are currently used for analysis of the containment response during this period.
The second phase is the period from hydrogen initiation through the end of.
core melt. .This phase, which progresses through various stages of degraded core conditions, is representative of the TMI-2 accident. Analyses of the containment response during this phase of the transient are performed using the CLASIX computer program which was developed by Offshore Power Systems.
These CLASIX analyses are the subject of this section and are discussed in
. the following pages.
The third phase of the transient is the period following vessel melt. This period is beyond the scope of these analyses.
1 2.1.2 CLASIX Base Case Analysis
-The parameters for.the base case analysis were selected by consideration of
- 1) available experimental data on hydrogen burn characteristics, 2) the 2-2 4
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potential effect of the containment engineered safeguards systems parameters, and 3) the containment geometry. The mass and energy releases from the break (steam, hydrogen, and fission products) were based on calculations by Battelle Memorial Institute at Columbus using the MARCH code. These parameters are summarized in Tables 1 through 3. The conditions inside the containment prior to the onset of hydrogen generation, including subcompartment volumes, temperatures, air and steam partial pressures, and ice mass, were determined from LOTIC analyses and the MARCH generated blowdown. These parameters are summarized in Table 4.
For the base case, it was assumed that ignition would occur at a hydrogen concentration of 10 percent by volume (V/o). Consistent with ignition at 10 V/0, the flame was assumed to propagate at 6 feet per second. Propagation was assumed to occur to any connected volume with a hydrogen concentration of at least 10 V/o. Ignition was assumed to occur at the center of the lower compartment, along the circumference of the dead ended region, or at the top of the upper compartment. Ignition in and propagation to any compartment with less than 5 V/o oxygen were suppressed. Consistent with ignition at 10 V/0, it was assumed that complete combustion occurs in any compartment in which a burn is initiated either by ignition or by propagation. These parameters are summarized in Table 5.
The spray system was modeled to provide a constant flow of 6000 gallons of 1250F water per minute to the upper compartment. The spray drops were assumed to have a diameter of 680 microns, a fall time of 10 seconds, and a heat transfer coefficient to the upper compartment atmosphere of 20 BTU /hr ft2 op, The spray system is automatically initiated 30 seconds after the containment reaches 3 psig. In this transient, spray initiation occurred prior to the beginning of the CLASIX analysis. The spray parameters are summarized in Table 6.
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The fan system was modeled to provide a constant flow of 80,000 cubic feet l per minute from the upper compartment to the lower compartment. About 0.55 percent of the fan flow'was directed to the dead-ended region of the lower compartment to represent the hydrogen skimmer system. The fan system is initiated 10 minutes after the containment reaches 3 psig. In this transient, fan initiation occurred prior to the beginning of the CLASIX analysis. The fan parameters are summarized in Table 6.
The ice condenser lower inlet and intermidiate deck doors were modeled based on the door representation in the Westinghouse Transient Mass Distribution (TMD) analyses for ice condenser plants. Both types of doors were modeled to act as check valves, preventing reverse flow. The lower inlet doors were restricted to a maximum opening of 55 degrees for this smail break transient. The door parameters are sumarized in Table 6.
Flow parameters for the flow paths between the various subcompartments are based on typical ice condenser containment geometry and are consistent with similar parameters used by Westinghouse on TMD calculations. Flow path parameters are summarized in Table 7.
The results of the base case CLASIX analysis, identified as JV900 in Tables 8 and 9, indicate that hydrogen will be ignited in a series of nine burns in the lower compartment over a period of about 3300 seconds beginning about 5000 seconds after accident initiation. One of the burns propagates into the ice condenser. Each burn in the lower compartment consumes about 100 pounds of hydrogen and the burn in the ice condenser consumes about 37 pounds of hydrogen, giving a total burn of about 900 pounds of hydrogen. For the first burn, calculated peak pressures were 26.5 psia in the lower compartment and 28.5 psia in the ice condenser and upper compartment, with a preburn pressure 2-4
l of 22.5 psia. Subsequent burns resulted in successively lower pressure peaks.
Peak temperatures of 22000F,12200F, and 1500F were calculated in the lower compartment, ice condenser, and upper compartment, respectively. Only small differential pressures occu. across containment structures during the transient.
As a result of the action of engineered safety features, such as the ice con-denser, air return fans and upper compartment spray, the pressure and tempera-i ture peaks were rapidly attenuated between burns with pressure returning to the pre-burn value approximately two minutes after the burn. At the end of the i transient, 7080 seconds after accident initiation, 650 pounds of hydrogen l
l remained distributed in the containment at a concentration insufficient for ignition and 300,000 pounds of ice remained in the ice condenser.
2.1.3 CLASIX Sensitivity Studies To determine the effects of ignition criteria and safeguards performance on containment response to hydrogen transients, a number of sensitivity studies were performed on the parameters that have been judged to have the greatest
. potential impact.
In the first sensitivity case, identified as JV901 in Tables 8,10 ar.d 11, the hydrogen concentrations for ignition and propagation were reduced from 10 V/o to 8 V/o. Based on experimental data, the burn fraction was also reduced from 1.0 to 0.5. All other parameters were the same as tho:e used in the base case. In this case there was a series of seventeen burns in the lower compartment, eight burns in the ice condenser, and one burn in the upper compartment. Although the number, magnitude, and distribution of the burns varies considerably from the base case, the total amount of hydrogen burned and the peak containment pressure during the transient do not vary appreciably from the base case. Peak temperatures in the lower compartment and ice 2-5 ,
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conder su are considerably lower than in the base case due to the smaller magnitude of the individual burns in these compartments.
In the second sensitivity study, identified as JV913 in Table 8, the hydrogen concentration for propagation was reduced from 10 V/o to 8V /o while the concentration for ignition was kept fixed at 10 V/o. For consistency with experimental data, the 8 V/o burns were restricted to a 50 percent burn fraction while the 10 V/o burns had complete combustion. All other parameters were identical to those used in the base case. In this case there was a series of three burns initiating in the lower compartment. All three burns propagated to the upper compartment and two of the burns propagated to the ice condenser. Again, although the number, magnitude, and distribution of the burns varias considerably from the previous cases, the peak pressures ano temperatures are similar to those calculated above.
In the third sensitivity case, identified as JVTC4 in Table 8, the hydrogen concentration for propagation was again reduced from 10 V/o to 8 V/o while the concentration for ignition was kept fixed at 10 V/o. For conservatism, all burns were assumed to have complete combustion. In addition, the fan flow rate was reduced from 80,000 cubic feet per minute to 40,000 cubic feet per minute. The results for this case are similar to the JV913 case, with an increased peak pressure and temperature in the upper compartment due to t.e F greater magnitude of the upper compartment burn.
In the fourth sensitivity case, identified as JV914 in Table 8, the flame speed was increased from 6 feet per second to 12 feet per second. All other paramters were identical to those used in the base case. The results of this case were very similar to those for the base case.
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In the fifth sensitivity case, identified as JV915 in Table 8, the flame speed was increased from 6 feet per second to 12 feet per second, the hydrogen concentrations for ignition and propagation were reduced from 10 V/o to 8 V/o, and the burn fraction was reduced from 1.0 to 0.5. All other parameters were identical to those used in the base case. The results of this case are similar to the first sensitivity case.
In the sixth sensitivity case, the fan flow rate was reduced from 80,000 cubic feet per minute to 40,000 cubic feet per minute with all other parameters identical to the base case. The results of this transient are almost identical to those for the base case.
In the seventh sensitivity case, the fan flow rate was reduced to zero in the CLASIX part of the analysis (i.e., from the beginning of H2 generation). All other parameters were identical to the base case. In this case, steam and hydrogen from the break push air out of the lower compartment reducing the oxygen supply belos the minimum 5 V/o required for burn initiation. As the transient continues, hydrogen accumul-: :s in the upper compartment and eventually ignites there.
This burn propagates to the ice condenser. The compartment and ice condenser burns cause a redistribution of the containment atmosphere, adding oxygen to the lower compartment and hydrogen tc the upper compartment. With the addition of oxygen to the lower compartment there is an independent lower compartment ignition which also propagates to the ice condenser and forces more hydrogen into the upper compartment in which hydrogen is still burning. The net result is a burn of approximately 1200 pounds of hydrogen in total, of which 860 pounds burn in the upper compartment. The peak calculated pressures are 92 psia in the upper compartment, 86 psia in the ice condenser, and 46 psia in the lower compartment.
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In the eighth sensitivity case, the ice condenser drain temperature was increased from 32 0 F to 132 0 F with all other parameters identical to those used in the base case. The results of this case are almost identical to i
'the base case results except for the ice remaining at the end of the 4
transient. - This indicates the . drain temperature is important to the ice condenser efficiency but not to its effectiveness.
! In the_ ninth sensitivity case, the initial ice mass was reduced by 1.17 x
> 106 pounds. Thus the ice mass input to the CLASIX part of the analysis was reduced from 1.67 x 106 pounds to 5 x 105 pounds with all other parameters
! identical to those used in the base case. This is a non-mechanistic study to determine the total effect of ice on a hydrogen transient. In this i
transient, ice melt out occurred during the second of a series of seven burns in the lower compartment. The peak containment pressure was about i '0 psi higher than in the base case.
h The remaining sensitivity cases were performed varying spray parameters, f Since spray operation is much more important for upper compartment burns
! than for lower compartment or ice condenser burns, these variations were
) performed for the upper compartment burn in the first sensitivity case, l i.e., the case witn ignition and propagation at 8 V/o hydrogen and 50 9
i percent burn fraction, identified as JV901.
.In the first' spray sensitivity case, the spray heat transfer coefficient
? 2 was reduced from 20 BTU /hr ft oF to 2 BTU /hr ft 0F. In the second spray sensitivity case, the spray temperature was increased from 125 UF .to 1800F.
In the third spray sensitivity case, the spray flow rate was reduced frorr 6000 gpm to 4700 gpm. In the fourth spray sensitivity case, the spray
' flow rate was increased from 6000 gpm to 9400 gpm. In the fifth spray-2-8 4 i
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sensitivity case, the spray flow was reduced to zero in the CLASIX part of the analysis. In the sixth spray sensitivity case, the spray drop diameter was reduced from 6t nicrons to 400 microns. In the last spray sensitivity case, the spray drop diameter was increased from 680 microns to 1000 microns.
The results of the spray system sensitivities are summarized in Table 12.
These results indicate that while spray temperature and some minimum flow rate are important, the remaining parameters are relatively unimportant for containment response to hydrogen burn transients. In the spray tempera-ture sensitivity case, the increased spray temperatnre resulted in an increase ambient pressure. The increased pressure required additional hydrogen to achieve the hydrogen concentration required for ignition so that a greater quantity of hydrogen was consumed in each lower compartment burn, and an upper compartment burn did not occur.
2.1.4 Summary and Conclusions The calculations described above represent the first attempt to perform a realistic assessmert of hydrogen transients in an ice condenser containment.
The geometry and engineered containment safeguards parameters used in the study were based on the Sequoyah containment design. Therefore the results i are directly applicable to the Sequoyah plant.
The results of this study indicate that over a wide range of cases, the Sequoyah containment pressure response to hydrogen transients would not cause containment failure.
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E TABLE 1 MARCH REACTOR C0OLANT ftASS AND ENERGY RELEASE RATES S2D SE00ENCE TIME MASS RELEASE RATE ENERGY RELEASE RATE (sec) (lbm/sec) (BTU /sec) 0.0 197.167 116722.67 2172 190.500 109728.00 2478 44.850 52295.10 3180 53.533 65471.27 3804 34.817 42615.60 4428 21.400 28419.20 4752 48.417 55582.33 5700 19.417 21824.33 6012 14.067 15825.00 6960 5.253 5988.80 7062 4.718 5388.34 7206 4.060 4693.36 l
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TABLE 2 MARCH HYDR 0 GEN GENERATION RATES AND TEMPERATURES S2D SEQUENCE TIME MASS RELEASE RATE TEMPERATURE (sec) (lbm/sec) (OF)
O.0 0.0000 61.24 3480 0.0000 61.24 3804 0.0413 66.56 4116 0.2600 1582.29 4428 0.7400 795.45 4752 1.0700 771.47 5700 0.4300 611.53 6330 0.2233 555.39 6648 0.1600 535.22 6960 0.1167 519.43 8070 0.0367 519.43 l
TABLE 3 MARCH FISS10tl PRODUCT Et4ERGY RELEASE RATES S2D SEQUEriCE T!!!E ErlERGY RELEASE RATE
-(sec) (BTU /sec) 1 l 0.0 0.0 3310 0.0 i 4116 1803 1
4428 4800 4752 6708 5376 7000 7080 7135 e
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TABLE 4 SUBCOMPARTMEriT PARAL 1ETERS*
CLASIX BASE CASE AfiALYSES S20 SEQUENCE LOWER ICE UPPER DEAD ENDED COMPARf1ENT** CONDENSER C0f1PARTf1ENT+ REGION 4
VOLUf1E (ft )
3 3.03 X 10 5
7.85 X 10 4 6.98 X 10 5 7.87 X 10 02 PRESSURE (psia) 2.53 3.70 3.62 3.62 fi2PRESSURE (psia) 9.56 13.98 13.67 13.67 H2 O PRESSURE (psia) 6.10 0.40 0.90 0.90 TEMPERATURE (OF) 171 75 98 98 ICE f1 ASS (1bm) 1.67 X 10 6 2
ICE HEAT TRANSFER AREA (ft ) 2.02 X 10 5 BASED ON LOTIC RESULTS INCLUDES f1ELTED OUT PORTION OF ICE CONDENSER
+ INCLUDES ICE CONDENSER UPPER PLENUM
TABLE 5 HYDROGEN BURN PARAMETERS CLASIX BASE CASE ANALYSES H2 V/o FOR IGNITION *10 H3 V/o FOR PROPAGATION 10 H2BURN FRACTION 1 02 V/o FOR IGNITION 5 0
MINIMU!1 02 V/o TO SUPPORT COMBUSTION
- PROPAGATION DELAY TIME LC-IC 12 sec IC-UC 5.5 sec UC-LC 60 sec LC-DE 12 sec
- EXCEPT IN THE ICE CONDENSER; ASSUMED NO IGNITION SOURCES AVAILABLE BASED ON A FLAME SPEED 0F 6ft/sec l
TABLE 6 SYSTEM PARAMETERS CLASIX BASE CASE ANALYSES Spray System Flow Rate 6000 gpm Temperature 125 F Drop Diameter 680 Fall Time 10 sec Heat Transfer Coef ficient 20 BTU /hr ft2 og Initiation Time S2D during LOTIC f
Air Return Fans flow Rate 80000 cfm Fraction of Flow to DE Compartment 0.0055 Initiation Time 52D during LOTIC Ice Condenser Lower Inlet Doors Ma>.imum Opening Angle (degrees) 55 Differential Pressure for Maximum Opening 0.0206 psi Maximum Flow Area 840 ft 2 Ice Condenser Intermediate Deck Doors Maxir.um Opening Angle (degrees) 85 Differential Pressure for "--imum Opening 0.493 psi i Maximur Flow Area 982.47 ft
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i TAR' E 7 FLOW RATE PARAMETERS
- CLAIX BASE CASE AriALYSES LC-IC IC-UC UC-LC DE-LC Flow Area (ft ) ** 2.2 108.6 Flow Loss Coefficient 1.12 2.26 1.5 3.0
- Baseo on Ti1D Models for ice condenser containments
- Function of door opening l
TABLE 8
SUMMARY
OF RESULTS S2D BURf1 SErlSITIVITY STUDIES JVTC4 JV900 JV901 JV913 52D JV914 JV915 Base Case (10/8%) (10/8%)
(103) (8~. ) (100/50% Burn) (100% Burn) _,
- Burns LC 9 17 3 3 9 .
IC 1 8 2 2 1 UC 0 1 3 1 0 Magnitude of LC e.100 n.4 5 mil 5 90 ,,100 Burns (lbm) IC 37 16-45 25-49 80 48 UC -
200 s230 430 -
Total H2Burned (lbm) s900 $1050 1100 950 900 H2 Remair.ing (Ibm) e650 s 500 450 600 650 Peak Temp. (OF) LC ,.2200 s1200 s1900 2100 2100 IC s1200 s 700 m 630 1500 1370 UC s 150 n.260 m 275 480 160 Peak Press,(psia) LC s26.5 s28.5 29 34 27 29 IC s28.5 s28.5 29 44 30 29 UC 28.5 S30.5 33 53 29 36 5 5 5 5 5 Ice Remaining (thm) 3x10 3.2x10 4.5x10 5x10 3.2x10 Figures 1-8 9-16 17-24 25-32 33-40 41-48
TACLE 9
SUMMARY
OF RESULTS S2D FAtt At1D ICE C0f1 DENSER SEfGITiv'ITY STUDIES JV900 JV902 JV903 JV904 JV905
[BaseCase). ( Fan)
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( Fan), (Lp_ss _ Ice)_ (Drain Temo)
- Burns LC 9 9 1 7 9 IC 1 1 2 0 1 UC 0 0 1 0 0 Maonitude of LC n.100 a100 s130 s100 Burns (lbm) IC 37 m 60 - ,, 3 9 UC - - - -
Total H2 Burned (lbn) s900 s900 s1200 s850 s950 H2 Remaining (1bm) s650 s650 350 s700 s600 Peak Temp. (OF) LC 2200 s2200 2370 s2400 s2000 IC 1200 $1350 2583 s2000 S1270 UC 150 s 160 1088 s 270 s 150 l I
Peak Press. (psia) LC 26.5 s26.5 46.4 a41 s26.5 IC 28.5 s26.5 86.4 s.41 s28.5 UC 28.5 s29.5 92.4 n.41 s26.5 5 5 Ice Remaining (lbm) 3x10 3.7x10 6.3x10 5 0.0 8.3x10 5 Figures 1-8 49-56 57-64 65-72 73-80
TABLE 10
SUMMARY
OF CASES CLASIX SPRAY PARAMETER SENSITIVITY STUDIES Case Number JV901 JV906 JV907 JV908 JV909 JV910 JV911 JV912 Spray flow Rate (gpm) 6000 6000 6000 4700 9400 0 6000 6000 Droplet Size /f 680 680 680 680 680 -
400 1000 Heat Transfer to Orop 20 2 20 20 20 -
20 20 (BTU /hr ft2 F)
Spray Temperature (F) 125 125 180 125 125 -
125 125 Figures 9-16 81-88 89-96 97-104 105-112 113-120 121-128 129-136
TABLE 11
SUMMARY
OF RESULTS CLASIX SPRAY PARAtiETER SEfiSITIVITY STUDIES Peak Pressure Peak Temperature Case (psia) (oF)
JV901 30.5 260.
JV906 34.0 340 JV907 This case did not have an UC burn.
JV903 33.8 270 JV909 30.9 255 s
JV910 52.3 930 JV911 31.5 255 JV912 32.2 280 I
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DUKE POWER COMPANY AN ANALYSIS OF HYDR 0 GEN CONTROL MEASURES AT MCGUIRE NUCLEAR STATION VOLUME 2 NOVEMBER 17, 1980
2.2 Summary of Analyses of McGuire Containment Response to Hydrogen Burn Transients 2.2.1 Introduction The calculations described in Section 2.1 represent the first realistic assessment of hydrogen transients in an ice condenser containment. Although the geometry and engineered safeguards parameters used in that study were based on the Sequoyah containment design, certain general results from those analyses are applicable to other ice condenser designs. Particular results applicable to all present ice condenser designs include: 1) ice,while beneficial, is not necessary for hydrogen control, 2) significant increases of upper compartment spray flow rate above some minimum value have little or no effect on containment peak pressure, and 3) some minimum fan flow is required to maintain containment integrity during a hydrogen transient. (This minimum fan flow has yet to be determined and may vary from plant to plant.) 2.2.2 McGuire Plant Parameters Input parameters for the McGuire CLASIX analyses include MARCH output data for the mass and energy releases from the break, LOTIC output data for con-tainment conditions prior to the onset of hydrogen production, and parameters for containment geometry and system descriptions. LOTIC data for the McGuire analyses are summarized in Tables 1 through 3. Parameters for the McGuire spray system and air return fans are given in Table 4. Flow path parameters for the McGuire containment are given in Table 5. Parameters not specifically identified in Tables 1 through 5 are identical to those used in the base case of Section 2.1. 2.2.3 McGuire Analysis l A series of calculations were performed for the McGuire containment design 2-10
in which both system parameters and burn parameters were varied. The first three cases were run with nominal containment safeguards of two fans and two spray trains operational. The fourth case was run with one fan and two spray trains operational. The remaining eight cases were run with one fan and one spray train operctional. In all cases, the flame speed was assumed to be 6 feet per second and burn initiation was suppressed in the ice condenser. The first four cases are summarized in Table 6. The first case considered for the McGuire plant, identified as JVD12, has burn parameters identical to those used in the base case of Section 2.1. Specifically, a burn is assumed to initiate at a hydrogen concentration of 10 percent by volume (v/o), to propagate to any adjacent compartment with a hydrogen concentration 10 V/o or more, and to have complete combustion. In the second of the McGuire analyses, identified as JVD13, the hydrogen concentration for ignition and propagation is 8 V/o and the burn fraction is 0.5. These burn criteria are identical to those used in the JV901 run of Section 2.1. In the third specific case for the McGuire plant, identified as JVD14, the burn parameters are the same as those used in the JV913 run of Section 2.1. In this case, ignition occurs at 10 V/o and propagation at 8 V/o hydrogen. The burn fraction is 1.0 for the 10 V/o 4 burns and 0.5 for the 8 V/o burns. The fourth case considered, identified as JVD15, is similar to the JVTC4 run of Section 2.1. In this case, ignition occurs at 10 V/o, propagation occurs at 8 V/o, and there is complete combustion for all burns. Cases five through eight are summarized in Table 7. The fifth case, identified as JVDC9 has burn parameters identical to those for the JVD12 run. The burn parameters for the JVD11 run, case six, are the same as those in the JVD13 run. The JVDC8 and JVDC4 runs have burn parameters identical to those used in the 2-11
T l ~ l JVD14 'and JVD15 runs, respectively. Cases five through eight all have ! McGuire minimum safeguards parameters. The last four cases are summarized in Table 8. Cases nine through eleven extend the analyses to ignition at 12 V/o hydrogen with the minimum safe- ! - guards.of one fan and one spray train operational. In case nine, identified as JVD10, propagation occurs at 12 V/o. The tenth case, identified as JVDC5, has propagation at 10 V/o and the eleventh case, identified as JVDC6, has propagation at 8 V/o. In all three cases, complete combustion is assumed for all burns. The last case considered for McGuire, identified as JDC7, has ignition at 14 V/o, propagation at 10 V/o, complete combustion for all
; burns and minimum safegurads of one fan and one spray train operational.
2.2.4 McGuire Results The results of the first four specific McGuire rur.s are sur,rnarized in Table ; i 6 and Figures 1 through 32. Comparisons with the corresponding cases from Section 2.1 indicate there are some minor differences in the hydrogen transients'in the Sequoyah and McGuire containments. These differences are attributed primarily to lower compartment geometry differences between the designs. In the McGuire cases, in general, there are increases in the , number of burns in the lower compartment, decreases in the amount of hydrogen consumed per burn in the lower compartment, increases in the number of burns propagating to the dead ended region of the lower compartment, and a small ( (-2 psi) increase in peak containment pressure. The results of the next four McGuire runs are summarized in Table 7 and Fi tures 33 through 64. Comparisons with the corresponding cases from Table l 6 indicate the effect of McGuire minimum safeguards. In the minimum safe-
' guards cases, in ganeral, there are increases in the number of burns in the 2-12 i
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- . _ . .. _ - ~ - . - . . - - _ . ,
. upper ' compartment with: corresponding decreases in the number of lower compart-ment burns, increases in.the peak pressures and temperatures particularly in
- the upper ccmpartment, and an increased ice melt during the transient.
The change in the' distribution of'the burns is attributable to the effects
~ of the lower fan flow rate in the minimum safeguards analyses. The lower fan flow rate results in a slower redistribution of hydrogen from the upper compartment to the lower compartment particularly following a lower compart-j ment burn. The net effect is that after several lower compartment burns, there
- is sufficient hydrogen buildup in the upper compartment for burn initiation or i propagation to occur.
The_ increased pressures and temperatures are attributable both to the change in the distribution of the burns and to the lower spray flow rate in the minimum safeguards analyses. The lower spray flow removes less energy during the burn. 1 Therefore, there is more energy and thus higher pressures and temperatures in the containment atmosphere at the end of the burn. This energy is removed by the combined effects of spray flow and fan forced circulation through the ice condenser. In these cases, more energy is being removed by the ice condenser T and thus there is greater ice melt than in previous cases. The results of the last four cases are summarized in Table 8 and Figures 65 through 96. In each of these: cases, there is a burn of at least 600 pounds of hydrogen in the upper compartment with resulting peak pressures of 85 psia or more. The last three cases are each characterized by a single burn that initiates in the lower compartment, propagates throughout the containment, and consumes 1000 pounds or more of hydrogen. These last four cases were under-i- taken when it was not clear at what volume percent hydrogen would consistently I ignite. Current information indicates that hydrogen will ignite and completely i 2-13 4 n_ . ,, . - - , , - , a,,--- mr, , , , - , . , . ~ - ,- .m , , -
i l l i l combust at levels below 10 volume percent. Therefore, these last four cases are considered to be very conservative and unrealistic. e l l l l 2-14
TABLE 1 SUBCOMPARTMENT PARAMETERS
- McGUIRE CLASIX AflALYSES S2D_SEgUENCE WITH 2 FANS AflD 2 SPRAY TRAlfiS OPERATIONAL LOWER ICE UPPER DEAD ENDED COMPARTMENT ** CONDENSER COMPARTMENT + REGION 3 5 VOLUME (FT ) 2.25 X 10 7.15 X 10 4 6.84 X 10 5 1.32 X 10 5 02PRESSURE (PSIA) 3.00 3.91 3.77 3.00 N2PRESSURE (PSIA) 11.35 14.79 14.25 11.35 H2O PRESSURE (PSIA) 4.78 0.43 1.11 4.78 TEMPERATURE (F) 160 75 105 160 ICE MASS (L8M) 1.58 X 10 6 2
ICE HEAT TRANSFER AREA (FT ) 1.91 X 10 5
- BASED Off LOTIC RESULTS AT 3480 SEC0flDS
** INCLUDES MELTED OUT PORTION OF ICE CONDENSER
+ INCLUDES ICE C0flDEriSER UPPER PLErlUM
TABLE 2 SUBCOMPARTMENT PARAMETERS
- McGUIRE CLASIX ANALYSES 52D SEQUENCE WITH 1 FAN AND 2 SPRAY TRAINS OPERATIONAL LOWER ICE UPPER DEAD ENDED COMPARTMENT ** CONDENSER COMPARTMENT + REGION VOLUME (FT )
3 2.25 X 10 5 7.18 X 10 4 6.84 X 10 5 1.32 X 10 5 02 PRESSURE (PSIA) 2.70 4.09 3.94 2.70 N2 PRESSURE (PSIA) 10.19 15.48 14.89 10.19 H2O PRESSURE (PSIA) 7.12 0.43 1.16 7.12 TEMPERATURE (F) 177 75 107 177 6 ICE MASS (LBM) 1.59 X 10 2 ICE HEAT TRANSFER AREA (FT ) 1.92 X 10
- BASED ON LOTIC RESULTS AT 3480 SECONDS
** INCLUDES MELTED OUT PORTION OF ICE CONDENSER
+ INCLUDES ICF CONDENSER UPPER PLENUM
TABLE 3 SUBCOMPARTMENT PAPAMETERS* McGUIRE CLASIX ANALYSES 52D SEQUENCE WITH 1 FAN AND 1 SPRAY TRAIN OPERATIONAL LOWER ICE UPPER DEAD ENDED COMPARTMENT ** CONDENSER COMPARTMENT + REGION 3 VOLUME (FT ) 2.47 X 10 5 7.19 X 10 6.84 X 10 1.32 X 10 02PRESSURE (PSIA) 2.62 3.95 3.85 2.62 N2PRESSURE (PSIA) 9.91 14.93 14.56 9.91 H2O PRESSURE (PSIA) 6.78 0.63 0.90 6.78 TEMPERATURE (F) 175 75 98 175 ICE MASS (LBM) 1.36 X 10 2 ICE HEAT TRANSFER AREA (FT ) 1.64 X 10 5
- BASED ON LOTIC RESULTS AT 3480 SECONDS
** INCLUDES MELTED OUT PORTION OF 'CE CONDENSER
+ INCLUDES ICE CONDENSER UPPER PLENUM
TABLE 4 SYSTEM PARAMETERS McGUIRE CLASIX ANALYSES SPRAY SYSTEM NUMEER OF TRAINS 2 FLOW RATE PER TRAIN (GPM) 3400 TEMPERATURE (F) 125 DROPDIAMETER(sC() 680 FALL TIME (SEC) 10 2 HEAT TRANSFER COEFFICIENT (BTV/HR FT F) 20 INITIATION TIME (SEC) DURING LOTIC AIR RETURN FANS NUMBER OF FANS 2 FLOW RATE PER FAN (CFM) 30000 INITIATION TIME (SEC) DURING LOTIC l HYDROGEN SKIMMER SYSTEM NUMEER OF FANS 2 FLOW RATE PER FAN (CFM) 3000 l l l
TABLE 5 FLOW PATil PARAMETERS
- McGUIRE CLASIX ANALYSES LC-IC IC-UC UC-LC DE-LC 2 ** **
FLOW AREA (FT ) 3.0 229.0 FLOW LOSS COEFFICIENT 2.05 3.04 1.5 5.1
- BASED ON McGUIRE TMD MODEL.
** FUNCTION OF D0OR OPENING.
TABLE 6 SU!?'ARY OF RESULTS McGUIRE CLASIX ANALYSES WITH 2 SPRAY TRAINS OPERATIONAL JVD12 JVD13 JVD14 JVD15 (10 V/0) .(8 V/0) (10/8 V/0) (10/8 V/0) (100% BURN) (50% BURN) (100/50% BURN) (100% BURN) (2 FANS) (2 FANS) (2 FANS) (1 FAN) NUMBER OF BURNS LC 10 22 4 4 IC 1 9 1 2 UC 0 1 3 1 MAGNITUDE OF BURNS LC 85 35 90 90 IC 40 20 25 50 UC -- 200 240 500 TOTAL H2 BURNED (LBM) 860 1100 1180 1100 H2REMAINING (LBM) 690 450 370 450 PEAK TEMPERATURE (F) LC 2000 1150 2000 2100 IC 1400 770 600 1700 UC 160 260 270 530 PEAK PRESSURE (PSIA) LC 27.5 29.5 31.0 35.0 IC 30.0 29.5 32.5 37.0 UC 30.0 30.5 35.0 57.0 5 ICE REMAINING (LBM) 3.2 X 10 3.2 X 10 4.3 X 10 4.1 X 10 FIGURES 1-8 9-16 17-24 25-32
TABLE 7
SUMMARY
OF.RESULTS McGUIRE CLASIX ANALYSES WITil 1 FAN AND 1 SPRAY TRAIN OPERATIONAL JVDC9 JVD11 . JVDC8- JVDC4 (10 V/0) (8 V/0) (10/8 V/0) (10/8 V/0)' (100% BURN) (50% BURN) (100/50% BURN) (100% BURN) NUM ER OF BURNS LC 6 19 4 3 IC 6 4 2 1 UC 1 2 2 1 MAGNITUDE OF BURNS 'LC 80 35 80 80
-(LBM) IC 15' 25 25 28 UC 525 190 260 480 TOTAL Hg BURNED (LBM) 1050 1100 -1050 900 H2REMAINING (LBM) 500 450 500 650 PEAK. TEMPERATURE (F) LC 2250 1350 2100 2000 IC 130 800 1550 1600 UC 1250 300 400 1000 l . PEAK PRESSURE (PSIA) LC 46 30 33 IC .43 46 30 36 UC 43 76 35 42 71 5
ICE REMAINING (LBM) 1.48 X 10 1.35 X 105 1.67 X 10 5 5 2.03 X 10 FIGURES- 33-40 41-48 49-56 57-64 k.
TABLE 8
SUMMARY
OF RESULTS McGUIRE CLASIX ANALYSES WITH 1 FAN AND 1 SPRAY TRAIN OPERATIONAL JVD10 JVDC5 JVDC6 JVDC7 (12 V/0) (12/10 V/0) (12/8 V/0) (14/10 V/0) (100% BURN) (100% BURN) (100% BURN) (100% BURN) NUMBER OF BURNS LC 3 1 1 1 IC 3 1 1 1 UC 1 1 1 1 MAGNITUDE OF BURNS LC 100 110 125 200 (LBM) IC 25 10 60 175 UC 600 635 600 800 TOTAL H2 BURNED (LBM) 850 880 880 1200 H2 REMAINING (LBM) 700 670 670 350 PEAK TEMPERATURE (F) LC 2350 2150 2150 2200 IC 130 1950 1950 2550 UC 1500 1400 1400 1900 PEAK PRESS (PSIA) LC 53 53 53 72 IC 52 53 64 93 UC 85 86 87 117 ICE REMAINING (LCM) 2.35 X 10 5 2.47 X 105 2.47 X 105 1.75 X 10 5 FIGURES 65-72 73-80 81-88 89-96
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