ML20088A630
| ML20088A630 | |
| Person / Time | |
|---|---|
| Site: | Pilgrim |
| Issue date: | 11/15/1983 |
| From: | Krueger J, Mondahl S BURMAH TECHNICAL SERVICES, INC. (FORMERLY CLOW CORP.) |
| To: | |
| Shared Package | |
| ML20088A629 | List: |
| References | |
| RTR-NUREG-0737, RTR-NUREG-737, TASK-2.E.4.2, TASK-TM NUDOCS 8404120315 | |
| Download: ML20088A630 (156) | |
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CLOW Clow Corporation 40 Chestnut Avenue 312 789-89oo Engineered Products Division Westmont,IL 6o559 103c 4-M M-l-2 3 - I t
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PURGE AND VENT VALVE OPERABILITY I
DISTRIBUTION con can 7*f[yf',, f QUALIFICATION ANALYSIS sueeuen
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PREPARED FOR anew s
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BOSTON EDISON COMPANY stecTacat JJ PILGRIM STATION # 600 UNIT 1 co m.sys.
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James E. Krueger Work performed under Bechtel Purchase Order Number -
P.O. No. 10394-M-119-1-AC, Rev. 1 Clow Job Number: 82-2739-01(N)
L This report covers Valve Mark Nos:
8" HBB-BF-AO-5035A 8" HBB-BF-AO-5035B 8" HBB-BF-AO-5036A 8" HBB-BF-AO-5036B BECHTEL POWER COPOR ATION JOB 10394 8" HBB-BF-AO-5042A SUPPLIER DOCUMENT STATUS STAMP 8" HBB-BF-A0-5042B 13 work may proceed.
8" HBB-BF-AO-5044B 2 C submit feal document. Work may proceed.
8" HBB-BF-A0-5044A 3 *3 Revise and resubmit. Work may proceed subp to resolution of incicated comments.
4 2 Revtse and resubmit. Wort may not proceed.
f 5 : Permtssion to proceed not reavited.
as.e.ne d ". E *.*"ae" N.E *m Yc."oe nIw**s os e or es ecies av ww suse.er. saa sees run re emode' trem fuS comphence with centractual esdageneae or sposes any "honee woneneceaireci AI C E
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DESCRIPTION OF CHANGES NO. I DATE BY BY BY AND PAGES REVISED r
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CERTIFICATION This is to certify that all valves (Tag Nos. 5035A & B, 5036A & B, 5042A & B, 5044A & B) have been evaluated for operabfif ty under the installed conditions indicated in supplied drawings and purchasing specifications. The information contained in this I
report is the result of complete and carefully conducted analyses i
and to the best of our knowledge is true and correct in all respects.
docu-The information presented in combination with the supporting I
ments referenced, represents a demonstrated qualification of the subject valves to the best of our knowledge for the required service application.
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Paper written and analyses by Steven M. Nondahl Design Engineer, Nuclear Clow Corporation hs.w Y L' w %
N/!6/ s3 James E. Krueger Design Engineering Mar.iger Clow Corporation M<
Ma as Paper reviewed and approved b Theodore E..Thygesen ' //
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L Professional Engineer Registration No. 062-034780 State of Illinois I
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TABLE OF CONTENTS Page LIST OF TABLES v
LIST OF FIGURES vi k
1.0 INTRODUCTION
1 1.1 Testing Performed 2
1.2 Qualification Method 5
A.
Environmental 5
B.
Structural (For Seismic and Other Loadings) 6 C.
Operability Under Flow 7
2.0 DESIGN OF VALVE AND ACTUATOR ASSEMBLY 10 2.1 Valve Design 10 2.1.1 Geometry 10 2.1.2 Materials 13 2.1.3 Operation 16 2.2 Actuator Design 20 2.2.1 Geometry 20 2.2.2 Actuator Design Materials 25 I
2.2.3 Actuator and Valve Operation 26 2.2.3.1 Actuators and Accessories Supplied 26 2.2.3.2 Actuator Output Torques 29 2.2.3.3 Operating Time 32 i
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TABLE OF CONTENTS (con't)'
Page
)
3.0 VALVE OPERATING AND INSTALLATION REQUIREMENTS 33 3.1 Valve Operating Conditions 33 3
' u 3.2 Valve Installation Configurations 35 4.0 VALVE STRUCTURAL INTEGRITY UNDER SEISMIC AND 38 OPERATION LOADINGS 4.1 Valve Stress Analysis 38 42 4.2 Actuator Tests 43 4.3 Valve / Actuator Test 44 5.0 VALVE AERODYNAMIC TORQUES 5.1 Model Tests 45 5.1.2 Tests With An Upstream Elbow 51 5.1.3 Downstream Piping Effects 55 5.2 Model Data Verification 56 5.3 Application of Model Aerodynamic Test to 57 Full Size Valve Operability 5.3.1 Valve Operating Times Expected in Service 57 5.3.2 Aerodynamic Torques For Valves As Installed 58 5.3.3 Conclusions Concerning Valve 73 I
Operability 5.3.4 NRC 21 Questions 74 L
6.0 VALVE SEALING CHARACTERISTICS 78 6.1 Normal Sealing 78 80 6.2 Long Term Sealing 6.3 Debris Effects On Sealing 81 6.4 Sealing Under Temperature Variations 82 L
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iv TABLE OF CONTENTS (con't)
Page
7.0 REFERENCES
L APPENDIX A APPENDIX B I
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v LIST OF TABLES PAGE TABLE TITLE 28 1
ACTUATOR ACCESSORIES 29 2
TORQUE DATA FOR PILGRIM AIR OPERATORS 32 3
VALVE BENCH TEST OPERATING TIMES 4
COMPARISON OF PILGRIM NUCLEAR SPECIFIC REQUIRE-MENTS TO GENERIC NUCLEAR QUALIFICATION DATA 39 40 4A
SUMMARY
OF ALLOWABLE STRESSES 5
TEST VALVE SCALED SIZES (CRITICAL ELEMENTS) 49 6
COMPARISON OF PRODUCTION VALVE TO VALVE MODEL 50 SIZES (CRITICAL ELEMENTS) 7 EMERGENCY FLOW, MAX CONTAINMENT PRESSURE 69 CHARACTERISTICS. STRAIGHT PIPE RUN 8
NORMAL FLOW CHARACTERISTICS, STRAIGHT PIPE RUN 70 (SHAFT UPSTREAM) 9 NORMAL FLOW CHARACTERISTICS, STRAIGHT PIPE RUM 71 (SHAFT DOWNSTREAM) 10 TORQUE FOR AS INSTALLED CONDITIONS FOR VALVES; 72 A0-5035A, A0-5035B, A0-5044A, A0-5044B.
11 TORQUE FOR AS INSTALLED CONDITIONS FOR VALVES; 72 A0-5036A, A0-5036B, A0-5042A, A0-5042B 79 12 VALVE SEALING CHARACTERISTICS L
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v1 LIST OF FIGURES FIGURE TITLE PAGE 1
TRICENTRIC3ALV$,0FFSETS 11 2
8" VALVE ASSEMBLY AND MATERIAL 15
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3 DISC WITH CLOSING FORCES APPLIED 18 i
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ACTUATOR SCOTCH YOKE DESIGN 21 TYPICALTORQUEOUTPUTFORDOUBLEAtkiNGSCOTCH 5
23 YOKE ACTUATOR 6
FAIL SAFE, SPRING RETUR!l ACTUATOR CESIGN 23 7
TYPICAL TORQUE OUTPUT CURVES FOR A SPRING 24 RETURN ACTUATOR 8
CALCULATED TORQUE DATA 732-SR80 30' 9
CALCUL ATED TORQUE PLOT 31 10 INSTALLED ORIENTATION OF 8" VALVES; A0-5035A, A0-5035B A0-5036A, A0-5036B 36 11 INSTALLED ORIENTATION OF 8" YALVES, A0-5042A, A0-5042B, A0-5044A, A0-5044B 37 12 VALVE ORIENTATIONS RELATIVE TO UPSTREAM ELBOW 53 13 THE HIGH PRESSURE VALVE MODELS WITH A.CONVE'RGENT ENTRANCE SECTION AND A VALVE-DISK OPENING ANGLE ~
54
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0F 80 s
N 14 SINGLE TEST VAltiE WATER TABLE EDERIMENTS WITH A VALVE-DISK OPENING ANGLE OF1800 AND A BACK s.
s 2
64 PRESSURE RATION OF 0.45 15 SIfiGLE TEST VALVE WATER TABLE EXPERIMENTS WITH A VALVE-DISK OPENING ANGLE OF 20 AND A BACK s'
65 PRESSURE RATIO OF 0.45 s
l 16 TWO TEST VALVE WATER TABLE EXPERIMENTS WITH AD 0
UPSTREAM VALVE-DISK OPENIrlG ANGLE OF 80,0A DOUNSTREAM VALVE-DISK OPENING ANGLE OF 80 f
ORIEisTATIOM 1, AND A BACK PRESSURE RATIO OF 0,45 '
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vii LIST OF FIGURES (con't)
FIGURE TITLE PAGE F
17 TWO TEST VALVE WATER TABLE EXPERIMENTS WITH 0
AN UPSTREAM VALVE-DISK OPENING ANGLE OF 80,
I A DOWNSTREAM VALVE-DISK OPENING ANGLE OF 0
60, ORIENTATION 1. AND A BACK PRESSURE RATIO OF 0.45 66 IS TWO TEST VALVE WATER TABLE EXPERIMENTS WITH AN UPSTREAM VALVE-DISK OPENING ANGLE OF 60.
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0 A DOWNSTREAM VALVE-DISK OPENING ANGLE OF 60,
ORIENTATION 1. DNA A BACK PRESSURE RATIO OF 0.45 67 19
'TWO TEST VALVE WATER TABLE EXPERIMENTS WITH AN UPSTREAM VALVE-DISK OPENING ANGLE OF 40 0 A DOWNSTREAM VALVE-DISK OPENING ANGLE OF 80,
ORIENTATION 1. AND A BACK PRESSURE RATIO OF 68 0.45 20 TWO TEST VALVE WATER TABLE EXPERIMENTS WITH AN UPSTREAM VALVE-DISK OPENING ANGLE OF 40 0 A DOWNSTREAM VALVE-DISK OPENING ANGLE OF 60,
ORIENTATION 1. AND A BACK PRESSURE RATIO OF 0.45 68 m
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1.
INTRODUCTION s
The Nuclear Regulatory Commission has, since 1979, been L
51ghly concerned about the operability of purge and vent valves during certain postulated occurrences. Their study in this area I
has shown that many valves were designed only to operate ander normal flow requirements. For a postulated loss of coolant accident, such valves may fail to close in the time required to prevent discharge of radiccc'iva gases to the outside environment.
Such a failure could exceed 10 ?FR 100 guidelines and present a significant hazard to the health of ps$rsons in the area.
NRC Branch Technical Position CSB 6-4 gives some background on operations of purge and vent systems and basic requirements for their design. For the valves used in such systems, further guidelines are provided in " Guidelines for Demonstration of Operabilit./ of Purge and Vent Valves", which was provided to nuclear plant operators by an NRC letter in September 1979.
This set of guidelines covers twenty-o".e points (less two) which are to be addressed by the plant operator. This paper addresses those items which may be answered by the valve manufacturer based i
I.
on the conditions provided by the plant operator for the postulated loss of coolant accident.
.This paper describes the de, sign of both Clow's Tricentric butterfly valve and the Bettis pneumatic actuator used to operate the valve. In, addition, descriptions of various tests performed E
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to determine flow and torque characteristics and application of this test data to the installed condition of the subject valves are presented. Information as to the structural integrity of the valve and operator assembly under seismic and other inplant loadings are also presented. This information, in combination with the supporting detailed technical reports (see 7.0 references),
represents a demonstrated qualification of the subject valves to the best of our knowledge for the required service application.
1.1 Testing Performed Clow became involved with design of butterfly valves specifically for purge and vent containment isolation early in 1981. A test program was initiated to deter-mine the mass flow and aerodynamic torque characteristics of the Tricentric butterfly valve design. Tests were per-formed for 12", 24", 48", and 96" scale model valves (scaled to 3" pipe size) in a straight pipe run for both uncnoked and choked flow regimes. Pressure ratios for choking, flow coefficients for mass ficw, and aerodynamic torque coefficients were determined in these experiments.
The experimental set ups met the ISA test requirements for compressible flow measurement. All measurements were automatically read, digitized, and recorded on magnetic
'L The obtained data was then evaluated by other tape.
computer programs.
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Subsequently, a computer program CVAP was developed using the measured data base to predict flow and torque values t
for full size valves in a straight run.
In the Spring of 1981, Clow personnel met with repre-sentatives of the NRC to review the test program to that i
point and to obtain recommendations for additional testing.
As a result, Clow and it's fluid dynamic consultant set up two additional programs to determine how the aerodynamic torque characteristics of the Tricentric valve varied with installed piping conditions.
For such conditions effects of both upstream and downstream piping elements (elbows, tees, reducers, etc.) were considered. From results of backpressure tests performed in the first set of exper-iments and water table studies previously done by Clow, it was determined that upstream piping elements would present a worst case condition. Further, due to the numerous types 0
of upstream elements (upstream elbows (mitered, 90, other angles, short radius, long radius), tres, reducers), a worst case had to be selected for evaluation. A 900 mitered e'1 bow was selected due to the fact that this element pre-
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sented the worst separated flow region at the inner corner and biased a major portion of the flow to the outer corner.
A second set of tests was developed to obtain information about the effect on each other of two valves in series (the common plant installed practice).
Due to the fact
that each experiment required an increasing amount of test combinations, the experiments were done in a phased approach.
The upstream elbow tests were performed first for a scale model of a 12" valve in 3 orientations relative to the elbow and at 3 spacings (2, 4, & 8 diameters) from the elbow. From the results a worst case was determined to occur at 2 diameters. Thus a scale model of the 24" and 48" were tested only at 2 diameters. Upstream elbow effects diminished significantly at 4 diameters and were barely detectable at 8 diameters.
From these results, the two valves in series tests As in were restricted to spacings of 2 and 4 diameters.
the elbow experiments, the worst case occurred at 2 dia-meters and at 4 diameters the results approached those for the single valva experiments.
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To substantiate the model tests and show the validity of scalint the model data to full size valves, Clow per-formed a choked flow operational test of a full size 12" valve with a pneumatic spring return actuator at Vought C'orp., Dallas, Texas, in November of 1981 (see the appen' dix i
for a basic description). The test showed that the valve conditinns, that I
would operate under the choked flow test h
mass flows were as predicted, and that use of the CVAP 1
program to predict torques was a conservative method L
(peak measured torque was approximately 65% of that pre-dicted). The test also incorporated a static 11.0 g load m
to the actuator simulating a severe seismic / hydro-It further validated the dynamic induced loading.
L directional effects of aerodynamic torque measured in I
the model tests (in the test all torques tended to close.
thevalve).
1.2 Qualification Method Clow provides certification of operability of valves pro-duced for purge and vent containment isolation service by The following items a combination of tests and analysis.
are considered and covered in this and supplemental reports.
A.
Environmental All portions of the Clow Tricentric is of com-pletely metallic construction other than stem The packings and the asbestos seal laminations.
valve seals by metal to metal contact between the The asbestos seal laminations used seat and seal.
to separate the SST laminations do contain a SBR binder which may degrade under radiation but the Further, the asbestos asbestos is uneffected.
laminations are shielded by the SST laminations
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and disc components. Although the asbestos may I
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become embrittled on the periphery, the valve will still perform its sealing function (see Radiation 17629-01).
Sensitivity Analysis Report Wyle
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The packings will perform their function under the required environment as long as they are replaced at recommended intervals.
Actuators used on the valves are qualified for the environment by the actuator manufacturer to codes, standards, or test procedures accepted.
by the valve buyer.
Structural (For Seismic and Other Loadings)
B.
Clow provides for each valve design, a finite element analysis of the valve structure and hand These calculations of selected components.
analyses show the valve to be constructed within ASME Section III requirements and that elements not covered by the code are designed with adequate Analyses can be found in this Qual-safety margin.
ification Report, the code required Design Report, The elements and the Structural Analysis Report.
considered by these reports include:
1.
Valve body 2.
Valve disc 3.
Valve disc shaft 4.
Valve disc shaft connection a.
Disc ear b.
Drive keys Dowel pin (retains shaft from hydro-c.
k dynamic end load only) i
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Actuator mounting structure L
a.
Adaptor flange
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b.
Bolting Actuators are qualified separately by the manufacturer by generic test results.
C.
Operability Under Flow Operability under maximum flow conditions is based on a combination of a bench test of each unit (timed test with no flow) and analysis of the torque characteristics. The bench test shows the closing cycle time when no aerodynamic torque is This data combined with conservative imposed.
(see assumptions below) calculations of the aero-dynamic torque is used to show the valve will close in the required time. Bench tests of actuators and valve assemblies include operation d_uring worst case conditions (minimum voltage, air supply, or maximum backpressure for pneumatic actuators if applicable).
The following method is used to show operability:
Determine no flow worst case operating time 1.
from bench tests.
L 2.
Using Clow program CVAP calculate aero-dynamic torques for straight pipe conditions.
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3.
Determine a torque modification factor based on the installed (from buyer prints)
L or a worst case upstream piping condition r
l using the mitered elbow or two valves in series test data.
Determine predicted torque values for all 4.
disc angles based on 2 and 3 above.
5.
Provide tabulation or plot of actuator output torque for all actuator angles.
Show that actuator output provides suffic-6.
ient margin to overcome aerodynamic and other torques (bearing, packing, disc wt.)
to close the valve.
From the above data, actuator type, and 7.
Vought full size test valve data, project a closing rate under the conditions analyzed above.
In the above calculations, the following assump-tions are employed:
Containment pressure is at a maximum a.
value and full flow is developed before valve starts to close.
L b.
The pressure downstream of the valve is atmospheric. In the elbow experi-ment it was noted that downstream e.us l
r elbows may choke before the valve for certain disc angles producing a higher
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L backpressure and lower torques.
Upstream piping components may produce I
c.
a less severe torque condition than the experimental element (mitered elbow worse than radius elbow).
d.
Torque coefficients used in the CVAP program are worse case values.
In the experiments a band of coefficients was observed with some dependence on pressure ratio. The high end of the band was used in the CVAP program.
Scaling of torques to larger size valves e.
by the D method may be largely conser-3
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vative as was shown by the Vought Test.
The net result of all such calculations and tests to date continue to show that the design and sizing of all components used in the valve or the actuator exceed the aerodynamic closure requirements based on design for suitable torques to seat and seal i
the valve.
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2.0 DESIGN OF VALVE AND ACTUATOR ASSEMBLY L
2.1 Valve Design r
2.1.1 Geometry The Tricentric valve uses a geometry that is unique not only This feature to purge valves but to butterfly valves in general.
gives the Tricentric functions 1 characteristics which are Thru use of a conical desirable in purge valve applications.
sealing surface with, the cone axis offset from the pipe axis and a rotation point selected so that it is offset from both the pipe axt_s and the seal plane, a metal to uetal seal can be obtained. (Fig. 1) The sealing is a result of normal forces acting between the sealing surfaces rather than sealing due to surface interference typical of other butterfly valves with elastomeric seals.
One of the major advantages of the conical seal design is This characteristic that it provides a non-jamming action.
results from controlling the cone angle so the angle of friction of the material is exceeded. This has been proven in actual tests similar to the test described here:
A 20 inch Tricentric wafer valve was closed by Then the t
applying 20,000 in.lbs. of seating torque.
This was repeated 3 unseating torque was measured.
times to determine an average value for the unseating em 9
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t The test was repeated with the seating torque torque.
increased by 10,000 in.lbs. increments until a maximum seating torque of 100,000 in.lbs. had been achieved.
During the entire test, the seat seal interface was dry (highest angle of friction) and no pressure was applied
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The smallest value of torque that could to the valve.
f be accurately measured was 1000 in.lbs. and at no time was more than 1000 in.lbs. required to unseat the valve regardless of the seating torque applied.
f Since the shaft is offset in 2 directions, one from the pipe f
axis and one from the seal plane, 2 performance advantages result.
The first is th'e sealing surface is continuous thru 360 degrees This elininates with no interruptions from the shaft penetration.
the leakage and wear associated with the shaft penetration areas.
The second advantage comes from the shaft being offset (eccentric)
This eccentricity produces unequal areas from the pipe axis.
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about the rotation point, so when the valve is closed and pressure is applied to the shaft side of the disc (normal direction), a This will result in increased sealing closing moment results.
forces between the seat-seal interface as pressure increases.
This force, in combination with the mechanical torque produced by the actuator, results in the tight sealing capability achieved i
A definite relationship between these with the Tricentric.
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2 offsets is required to provide a valve that has no binding or f
interference problems as the seal is rotated out of the seat.
This relationship is determined analytically to provide the best performance without overdesigning the valve components.
All of these features have been incorporated into the lugged wafer i
body that results in a very rugged and sturdy valve design capable.
of meeting or exceeding all the requirements set forth in most specifications.
2.1.2 Materials A complete list of valve component materials used on Bechtel Purchase Order Number 10394-M-119-1-AC, Rev. I may be found on the General Arrangement Drawing (D-0741) which follows this section.
Since purge an,d _ vent valves must perform safety related functions not only during normal conditions but C.so during and after upset, emergency and faulted conditions, the material Because the valves selections were based on a worst case event.
are required to prevent discharge of radioactive gases to the outside environment during a LOCA, the seat and seal materials '
are critical to the operation of the valves. During normal operation the valves are exposed to the air in the containment and outside air, but during a LOCA the media may be made up of steam, air, and boric acid, all of which may be radioactive and i
The seat material selected for this at elevated temperatures.
application was SA240 316L SST. The 316 grade was selected due W
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to its corrosion resistance and ability to withstand all of the The L 9
possible medias that may come in contact with the seat.
t grade of 316 SST was further specified because the seat is welded i
to the body (SA516 GR 70) and the L grade has a lower carbon content that will reduce the carbide precipitation in the heat affected zone Both The seal is a laminate of 316 SST and asbestos.
of the seat.
The 316 SST was chosen in the laminants are 1/32 inch thick.
The asbestos
" straight" grade since no welding is done on the seal.
The used is made of John Manville style 60 or equal material.
laminated type seal was selected for its ability to seal with less The laminate allows torque thsn would be required for a solid seal.
each SST member to act independently and to conform to the contour The asbestos of the machined seat as seating torque is applied.
to act independently but member not only allows each SST member also reduces the seal area in contact with the seat and therefore, results in application of higher normal stresses to the seal for any given seating torque.
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2.1.3 Operation The operation of the Tricentric valve is extremely simple f
i since there are only 2 moving parts, the disc assembly and the k
The valve operates by changing the position of the disc shaft.
relative to the seat. This is accomplished through the application or control of torque on the valve shaft through the entire f
operating range of 90 degress. (Zero degrees being fully closed and 90 degrees fully open). There are seven different torques of importance that the valve will encounter depending on the disc The valve shaft position or change in position required, if any.
must be designed to withstand the worst case combination of these f
operating torques without being overstressed. These torques are described in a random sequence since they may occur in different sequences during actual valve operation.
1.
Bearing friction torque is the result of the flow or pressure forces acting on the disc which are transmitted to the bearing through the shaft which supports the disc.
l The bearing friction torque is proportional to these forces acting on the disc and the coefficient of friction between the shaft and the bearing materials. Bearing friction f
torque must be overcome anytime the disc is required to change position.
2.
Packing or seal friction torque is the result of the
[_
normal forces the packing exerts on the shaft. These normal t
{!L l
I
forces are due to the packing gland force and the internal valve pressure. The packing gland force is required to effect a shaft seal. The packing friction torque is also l
dependent on the coefficient of friction between the packing and the shaft material. Packing friction torque must also be overcome when the disc is required to change positions.
3.
-PMi (Pressure Area 'lethod) toique is the torque produced by the differential pressure acting on the unequal areas of either side of the eccentric shaft centerline. (Fig. 3)
The PAM torque is therefore ' dependent on the valve size, shaft eccentricity and the differential pressure.
l Depending on which side of the disc the pressure is applied,
(
the PAM torque may aid seating or unseating of the valve disc.
4.
Seating torque is the amount of torque required to develop the normal forces between the seat and seal to effect
{
a tight closure. Seating torque is dependent on the sealing materials, seal thickness, valve geometry, valve size, differential pressure and leakage requirements. As seen in Fig. 3, as the valve is seated by applying a closing moment T, the normal forces Rr; will increase. Since the seal 1
angle varies around the seal circumference, Rr; also varies, thus the point uber: Rii is a minimum must be loaded sufficiently to effect a seal. Sealing characteristics will be further discussed in the section under Valve Sealing Characteristics (Section 6.0).
f~
(-
l-f l
CONE AXIS DISC Axis f
ECCENTR'ICITY(E)
I T
CLOSt Rn n
/
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/-
I DISC / SEAL 1 R,\\
/
I Rn l
i 1
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T1 = Closing torque applied by actuator P = Force equivalent to disc pressure loading Rg4 = Normal seat reaction ' force due to torque application RT = Tangential seat reaction force due to disc notion (friction) t DISC WITH CLOSING FORCES APPLIED FIGURE 3 I
5.
Unseating torque is the torque required to move the L
seal out of contact with the seat. Unseating torque is a
also dependent on the sealing materials, seal thickness, valve geometry, valve size, differential pressure, and also the seating torque. As described in the section under Valve Design, when no pressure was applied to the valve, the unseating torque was small relative to the applied seating torque. However, when pressure is applied to the shaft side of the disc, not only does the normal force (RN) increase but also the frictional force (R )
T which resists opening.
This increase in frictional force i
may exceed the PAM torque. Thus an actuator is selected to provide an output torque greater than PAM torque.
6.
Weight offset torque is the result of tne C.G* of the disc being displaced from the rotation point. The weight offset torque is proportional to the disc weight, shaf t eccentricity, disc position, and the valve installation position. On small size valves the weight offset torque L-is generally an insignificant amount since the disc weight is sd small.
7.
Fluid aerodynamic torque is the torque due to inter-action of the flowing media with the valve disc. This is covered in detail in Section 5.0.
O
- Center of Gravity 9
As seen in the Vought Corp. Test Report (Reference 7.0 B-1)
[
the running torque was approximately 1000 in.lbs. This is seen in Fig. 8 Run 1 and Fig.15 Run 8 with no flow through the valve.
f This running torque is a combination of bearing, packing, and l
weight offset torque values.
The unseating torque may also be seen, which was approximately 1500 in. Ibs. when a seating torque of approximately 18,000 in.lbs. was used to close the valve with a 80 psig air supply to the actuator.
2.2 Actuator Design 2.2.1 Geometry The basic actuator is a device by which air pressure is converted to thrust through a linear cylinder and then converted to a rotary (900) motion through the use of a " Scotch-Yoke".
This device has a torque output at the beginning and end of its stroke, commonly referred to as breaking torque, that is approx-imately twice the magnitude of the torque output at the center of its stroke, referred to as running torque. The basic design u
of the scotch yoke can be seen in Figure 4.
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FIGURE 4 - ACTUATOR SCOTCH YOKE DESIGN From the above it can be seen that the moment arm varies
(
throughout the stroke. By geometric design the moment arm length at the beginning and end of the stroke can be found by dividing 0 or.707.
the moment arm length at the center by the cosine of 45 f
By performing this arithmetic it will be found that the moment arm at the beginning and ending is roughly one and one half times the moment arm at the center.
By design the " Scotch Yoke" mechanism multiplies the force
(
imparted by the piston thru a reaction from the bearings.
As pressure is applied to the piston the pin or roller is moved l.
against the slot in the yoke causing the rod to act on the bearing.
h To keep the action in a static condition a force or resistance must be applied to the yoke equal to the force from the bearing.
The total resultant force then beccmes the piston area times the 1
pressure applied divided by the cosine of 45.
eup s
The torque output from a " Scotch-Yoke" mechanism can be calculated as follows:
TORQUE AT EENTER OF STROKE i
i T=PXAXM f
Where:
T = Torque in in-lb l
P = Operating pressure in p.s.i.
MA = Moment arm in inches at center
[
A = Area of the piston in square inches TORQUE AT BEGINilING AND END OF STROKE MA T=FX tos.45" f
Where:
T = Torque in in-lb PyA F = Resultant total force in po inds =
= Moment arm at beginning and end of A
{
g,
- 45o stroke in inches.
A graphic representation of the torque output as a function
(
of di.sc position can be seen in Figure 5.
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r if I
r break torque f
5 l
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if running torque 3o L
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rl ROTATION FIGURE 5-Typical. torque output for double acting scotch yoke actuator.
(
Since thrust is converted to rotary motion, a spring is used
{)
opposing the air cylinder to provide a " Fail Safe" actuator. The
" Fail Safe" actuator is capable of performing its safety related f
function in the event of a loss of either the air supply or the control signal to the solenoid valve which controls the air supply l
to the actuator. The basic construction of the " Fail Safe" actuator is seen here.
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l FIGURE 6 - Fail safe, spring return actuator design
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2.2.2. Actuator Design Materials The Bettis actuators used for this job are 732-SR80-S series actuators. These were further specified to be the M f
version for nuclear service and qualified per IEEE 323-1974, IEEE 344-1975, and IEEE 382. Also, upgraded seismic qualifi-cations are provided based on Patel ReportPEI-TR-83-29, Rev. A with Addendum I and II. These actuators incorporate use of special materials for nuclear service as listed below.
Special Material:
Grease - Mobil 28 Seals - Ethylene Propylene Internal cylinder coating - Molybdenum disulfide Yoke pin and rollers - Ryton coated be w
3 m
i M
O j
2.2.3 Actuator and Valve Operation 2.2.3.1 Actuator and Accessories Supplied A complete list of all accessories specified for use on each
[
valve can be found in Table 1 and each is further described here.
An Asco solenoid valve is used on each actuator to control the air supply to the actuator and, to " dump" the air in the cylinder which allows the valve to open or close as required. The solenoid
~
l valves are 3 way, internal piloted diaphragm valves. The solenoid
(
valves are controlled by a coil. When the coil is de-energized by intentional or faulted conditions, the cy'linder port is allowed to discharge through the exhaust port and thereby allow the spring When the coil return actuator to perform its required function.
is energized, the supply pressure is directed into the cylinder f
and rotates the valve in a direction opposite to spring induced The solenoid valve model recommended for use is a rotation.
NFL831664E. This valve is designated for use in nuclear power applications which consists of providing IEEE compliance and a waterproof solenoid closure.
It is a high flow valve which has 1/2 in. NPT ports and a 5/8 in. ori.fice. All elastomeric materials of construction are Ethylene Propylene material for the NP unit.
I
- r me L
i
(
F ie Since the output of the unit is a function of the thrust r
applied, a new torque output curve must be used because the air cylinder not only moves the " Scotch Yoke" but must now also r
}
A typical torque output graph is shown here s
compress the spring.
for both the pressure stroke and the spring return stroke.
i values will be presented A description of actual output torque in the Operation Section.
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Yoke Arm Angle FIGURE 7 - Typical torcue output curves for a spring return actuator
[
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I L1;it switch;s are also provided. These are mounted;0n the actuator to indicate full open or closed position. One of each model number switch is supplied, one for the open posit'ic.1 and.the other for the closed position. The switch model numbers are iamco EA180-31302 and EA180-32301 which are DPDT swit'ches with 2 NO'and s~
s 2 NC contacts and are quick make,9 Ekgeaktype. The switches i
meet NEMA 1, 4, and 13 and IEEE 344, requiremets. Both switches I
use the same lever arm which is a Namco model ELO10-53337.
Other accessories to the actuator include a Fisher typy 95H l
regulator A V6-1/2-40-CI. Rosedale Filter, A1008 CHN,F Hoffman t
Junction Box Anaconda flexible liquid tight conduits'; snd various
[
(
~
tubing, pipe, and electrical fittings andl appropriate mo:inting I
ha rdwa re. All items' were not supplied with full n'iclear IEEE qualifications. The, unit a's sold will perform its intended function
(
to fail close even if failure of unqualified componer,ts occur.
,{
t Further, seismic tests performed ur.-d Clow Job 82-2053(N) did show such unqualified' items performed their intended function under the
\\
(
required vibration level of the ' specification as they were mounted
\\
for the test.
~
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f The air'oharators are manufacthed in aSyordance with Bettis -
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1 Engineering De;ign Standards.
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TABLE 1
~
Actuator Accessories for Each Unit Fall-sa fe Asco Namco limit switches Bettis Rotation Fail-Solenoid and lever are Valve Clow Actuator (viewed safe Valve Model Nos.
i Size Mark Job Model act, end Valve Model (1 closed position switch)
Other Items fin.) Nos.
No.
No.
of unit) Position No.
(1 open position switch)
(each unit) l i
- 1. RECOMMENDED EQUIPMENT 8"
5035A 82-2739(N) N732-SR80 CW Close NPX831664E*
EA170-31302 L.S. 8 Fisher type 95H 50358 regulator 5036A EA170-32302 L.S. I Rosedale Y6-1/2-40-C{
50368 filter 5042A ELO10-53337 L.A.
Misc fittings and 50428 electrical accessori 50448 5044A N732-SR80-M3-5 l
II. SUPPLIED EQUIPMENT 8"
5035A 82-2739(N) N732-SR80-S CW Close NPL831664E*
EA180-31302 L.S. I Fisher type 95H 5035B regulator 5036A EA180-32302 L.S.I Rosedale Y6-1/2-40-C1 50368 filter 5042A EL010-53337 L.A.
Misc fittings and 50428 electrical accesso?
5044B 5044A N 732-SR80-M3-5
- Number difference related to Asco numbering change between when Clow placed order and when units were received.
X indicated special which called for extra length leads
. L indicates extra length leads
- EA170 units are qualified for outside containment service EA180 units are qualified for inside containment service
e 2.2.3.2 Actuator Output Tarqu;s For this job, the Bettis Actuator Company ran tests of and L
provided certified reports confirming the ending torques of each unit. The tests were performed in both the spring and pneumatic directions, and the results are tabulated in Table E.
There is good correlation between the data and theoretical values.
TABLE 2
, TORQUE DATA FOR PILGRIM AIR OPERATORS
- I Unit, Mark i Spring Supplied Seating Torque (00 Rotation) in-lb A0-5035A 9,572 A0-5035B 10,515 A0-5036A 10,432 A0-5036B 10,687 A0-5042A 9,263 A0-5042B 10.470 A0-504aB 10,266 A0-5044A 11,032
- Actuator units were not assembled to valve when torque tests were run
{I The torque plots provided in this section represent the calculated output torque of the actuators for the spring and various supply pressures shown. The graphs which follow show how the torqt.c output varies for the pressure stroke as a function of upply pressure.
It can also be seen that the spring output torque is not a function I
of supply pressure. The graphs also demonstrate that the output torque (pressure on spring stroke) is a function of yoke position.
The graphs provided are based on the numerical data provided.
i L
M
732'S%Z a
f D
DA"A E I
I CYLINDER DIAMETER Cin)=
7.03 CENTER OR TIE BAR DIAMETER Cin)=
0.000 PIST0H ROD DI AMETER Cin)=
2.125 HUMBER OF PISTONS =
2 MOMENT ARM (in)=
3.375 SPRING LOAD A C1bs)=
1737 SPRING LOA 0 8 C2bs)=
4247 BREAK EFFICIENCY C )=
75 87 RUHHING EFFICIENCY C1)
=
78 ENDING EFFICIEHCY CI)
=
70 80 90 100 PRESSURES (psi)
=
CCTUATOR TYPE C8-1,HD=2,T.TR=3, =
2
~
f YDKE ARM SPRIHG PRESSURE PRESSURE PRESSURE PRESSURE EF F I CIEHCY ANGLE TORQUE TOROUE
PRES.
(degrees)
Can Ib)
C 70) psi
( 80) psi
(
- 90) psi
( 100)pst I
0 10060 16541 20286 24031 27776 78 75 5
9511 13881 17179 20477 23775 80 78 10; S051 11948 14913 17878 20843 82 80 15 8687 10508 13222 15937 18651 83 82 20 8418 S416 11942 14468 16994 85 83 25 8240 8578 10965 13351 15737 86 84 30 8149 7933 10219 12504 14790 8'6 85 35 8146 7438 9656 11874 14092 87 86 40 8232 7061 9242 11423 13604 87 87
?
45 8412
- 6784 8955 11126 13297 87 87 '
50 8697 6591 8779 10967 13155 87 87 l_
55 Sici 6471 8704 10938 13171 86 87
~
SC 9648 6417 8726 11036 13345 85 86 65 10366 6424 8844 11264 13684 84 86 70 11311 6489 9061 11633 14205 83 85
,)
75 12544 6605 S381 12157 14933 82 83 80 14172 6765 9812 12860 15907 80 82 85 16355 6955 10363 13771 17179 78 80 90 19350 7133 11033 id*
t
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Page 32
'f 2.2.3.3. Operating Time r
'f Bench Test - The following is a summary of the operating times
[
recorded during the operational test performed on each valve.
The tests were performed using a 100 PSIG air supply. There was
(
no flow through the valve during this test.
f TABLE 3 Velve Bettis Opening Closing Mark No.
Size Actuator Time Time of Valve (inch)
Model No.
Sec.
Sec.
A0-5035A 8
N732-SR80-S 4.3 2.7 A0-5035B 8
2.6 2.94
(-
A0-5036A 8
2.64 2.49 A0-5036B 8
5.3 2.1 A0-5042A 8
3.29 2.44 g
A0-5042B 8
2.94 2.54 1
A0-5044B 8
3.89 2.71 A0-5044A B
N732-SR80-S-M3 2.87 2.46 I
I Il 1:
4 m
j Page 33 f'
3.0 VALVE OPERATING AND INSTALLATION REQUIREMENTS 3.1 Valve Operating Conditions f
The valves were designed to fail close (activation of f
solenoid valve to allow unit to close to be provided by Boston Edison) and to allow closure and sealing against a 56 PSI f
I 1
differential applied to the shaft side of the disc. Sealing was also to be provided for a differential pressure of 56 PSI applied to the clamp ring side for in plant test purposes. At the request of the buyer, leakage tests were also performed at 5 and 25 PSI differential from each side.
Seismic and other loading conditions for operation are as
(
indicated in the specification. Actuator qualifications for environmental and seismic are covered by previous actuator quali-fications supplied by the manufacturer (Bettis) and added seismic tests performed in accord with NTS (National Technical System)
Test Plan No. 528-0951 for Clow Job No. 82-2053(N) (see References Sect. 7.0).
The Bettis units have been tested to the required j
level and have demonstrated their ability to function as required.
For the subject valves the following operating and design conditions are applicable.
Operating conditions:
Normal operating pressure
= 1.5 PSI Normal operating temperature = 65-1940F 5700 SCFM I
Normal operating flow
=
IL L
j Page 34 4
r Design conditions Max. operating pressure body only = 285 PSIG 0100 F 0
- Max. pressure differential disc
= 56 PSID Max. temperature
= 350 F 0
~
Required Torque to seat
= 7681 in-lb.
Failure mode
= Fail close f.
Allowed leakage
=.26 cc/ min air N
0 56 PSID
(
t.
- Bidirectional sealing provided to 56 PSID only I
f b
,1 TI I
I t
ri I~
Page 35 L
I 3.2 Valve Installation Configurations In addition to the pressure and flow conditions specified in 3.0, the valve. performance is affected by the as installed orientation.
Upstream and downstream, tees, elbows, reducers, and other valves can f
affect the aerodynamic torque characteristics of butterfly valves.
l These effects are discussed in Section 5.0.
The installed config-l l
urations for the subject valves as derived from Bechtel drawings i
SK-P-001, Rev. F, Job No. 10394-105, are summarized in Figures 10 and 11 l
.I
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l PURGE LINE TO ORYWELL E
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gg 18"
$V S
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AO-50358 7
h i
22" g
-8L 20" Q
AO-5035A ORIENTATED 45" FROM AS SH0HN m
AO-5036B g 20" GRIENTATED
-8 45' FROM I-AS SHOWN 22"
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-2 0 8---
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- GU R E
- .0 PURGE LINE INSTALLED ORIENTATION OF 8" VALVES, A0-5035A:
TO TORUS Ao-503ses Ao-503sAs a Ao-503ss.
Page 37 VENT LINE N
f TO TORUS E
dM
$V ign 3
13" AO-5042A @
i
}
14" I
A0-5042B Q 20" 8"
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- 20'L VENT LINE TO DRYWELL
$AO-5044A AO-50448 a
20" h
8" LOC OH }
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=!
$ A0-5044A ORIENTATED
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120" FROM AS SHOHN.
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INSTALLED ORIENTATION OF 8" VALVES, A0-5042As
'L A0-5042B> A0-5044AJ & A0-50448, e
Page 33 4.0 VALVE STRUCTURAL INTEGRITY UNDER SEISMIC AND OPERATIONAL
~
LOADINGS l
{
Operability of the subject valves has been demonstrated by a combination of testing and analysis in accord with the design specification. Separate reports have been prepared and provided i
demonstrating suitability of valve components and the assembly.
A listing is provided in the References (7.0) at the end of the report. This section summaries the results of such tests and analyses in meeting the conditions as presented in Section 3.0.
4.1 Valve Stress Analysis Valve stress analysis was performed by Patel Engineers, Huntsville, Alabama for the subject valves. The analysis was made using the ANSYS finite element computer program developed by Swanson Analysis System, Inc., Houston, Pa. This public domain program has had a sufficient history or use to justify its appli-cability and validity. The analysis performed compares the nuclear specific requirements of the Pilgrim Job, Report PEI-TR-833700-1,
~
to an already performed worst case generic qualification report I
for a Clow 8" Wafer Stop Valve, PEI-TR-83-24, Rev. A.
The com-parison of key elements in these reports is shown in Tables 4 and 4A.
t O
e 6
4 4
Page 39 m
p TABLE 4 COMPARISON OF PILGRIM NUCLEAR SPECIFIC REQUIREMENTS TO f
GENERIC NUCLEAR QUALIFICATION DATA (REFERENCE 1)
I l
LOADINGS GENERIC PILGRIM Pressure l
285 p
Shell (psig) 285 Seat (psid) 75 56 I
Torque (in Ib) 16643 9056 Seismic Acceleration NS (g) 7.0 4.5
[
f Vertical (g) i 7.0 EW (g) 7.0 l
4.5 4.5 j
1 i
I l
L'
' OPERATOR l
i 2
I i Weight (lb) i 550 360 l
Center of Gravity p
X (in) 10 10.81
{
Y (in) 10 1.01 i
2 (in) 18 3.99 FREQUENCY fo (Hz) 59.5
! f >_ 33 Hz o
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EVALUATIO*1 AGAI:lST ASME Section III ASME Section III
[
Design and Level A Design and Level A
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q
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U Table 4A Summary of Allowable Stresses LOC /.T I Ot1 HATERIAL ALI,0WABLE STRESS STRESS REPORT IN WHICH STRESS (psi)
VALUE ITEM IS ANALYZED **
RATIO (PER ASME SECTION (psi)
/ SEISMIC LOAD LEVEL III, TABI.ES 1-7.1 TilROUCll I-7.3)
Valve Eody SA 516 17500 5319 Generic 7.0 g 0.30 CR.70 Disc SA 516 17500 4947 Generic 7.0 g 0.28 CR.70 Drive Shaft SA 564 34550 18794 Generic 7.0 g 0.54 Type 630 11-1100 operator Adapter SA 516
'17500 4936 Pilgrim 4.5 g 0.28 Plate CR.70 Adapter Plate SA 193 25000 14569 'k Pilgrim 4.5 g 0.08*
Balts CR.B7 4929 T operator / Adapter SR 193 25000 103215k Pilgrim 4.5 g 0.1g*
m Dolts CR.B7 10767r E
m Cover Plate SA 516 17500 10492 Generic 7.09 0.60 CR. 70 Cover Plate Bolts SA 193 25000 7000Ek Generic 7.0 g 0.01*
CR.B7 102 T
,, Per ASME,Section III, Appendix XVII, Subsubarticle 2460.
r---.4.
no-o.+.4e o +n1 orf To Al-?4. Pilorim Report 'is Patel PEI-TR-833700-1
cy Page 41 Q
{I The Pilgrim seismic analysis specifically addresses the operator adaptor plate, adaptor plate bolts, and operator /
adaptor bolts since these were determined to be the weakest items. The other items are covered in the generic analysis.
The conclusion that can be drawn is that the structural integrity of the.ubject valve assemblies fully meets the requirements of Bechtel Design Specification 8031-P-144, Revision 2 and ASME Section III,1980 Edition.
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Page 42 k
4.2 Actuator Tests Two size Bettis actuators were tested for the Bechtel
[-
1.imerick Project under Clow Job No. 82-2053(N) in accord with j
National Technical Systems (Saugus, Ca. facility) Procedure 528-0951. The units tested were as follows:
Unit 1 NT-820-SR4-S Spring ending torque = 93,098 in lb Pressure torque + =
178,160 in Ib r
Unit 2 NT-312-SR5 Spring ending torque = 5,810 in lb Pressure torque + = 31,263 in lb
+ at 80 PSIG pressure to air cylinder The units were both spring return fail closed units and were representative of the line of actuators which would be used on containment purge and vent valves. The units were tested for baseline performance, subjected to OBE and SSE levels in accord with the procedure and specification, and then were operationally tested. The units proved to be operable both during and after
\\,
the required tests and upon inspection showed no signs of noticeable wear. Successful operation of these units in combin-ation with previous generic qualification for enviromental i
conditions generically qualifies the N732-SR80 units used on this job. (Note an addenda is provided to the report justifying
[h similarity, see References, Section 7.0) t
Page 63 r
I 4.3 Valve / Actuator Test
(~
In addition to the tests performed on the preceding
.i actuators, a 6" valve in combination with the NT-312-SR5 f
actuator were statically loaded and tested for operation.
The valve operated as required during the tests. This l
demonstrated that the valve / actuator interface for the 6" valve was sufficiently rigid to allow the unit to perform its safety related function. This test further qualifies the subject 8" valve based on Table C-1 of Bechtel Spec.
8031-P-144 t
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4 ST[T'
5.0 VALVE AERODYNAMIC TORQUES Depending upon the valve design, actuator sizing, inplant installed configuration, and operating conditions, aerodynamic torque may be of major concern to valve operability. The i
magnitude and direction of this torque, which is produced by flow of the media over the disc, depends on severalifactors:
I 1.
Disc shape 2.
Pivot shaft location 3.
Magnitude of differential pressure across the valve 4.
As installed upstream piping elements (elbows, tees, etc.) including distance and orientation relative to these items.
l 5.
As installed downstream piping elements (elbows, tees, length of pipe runs, etc.) including distance and orientation relative to these items.
6.
Angle of the disc Clow has done numerous tests of scale models of the f
Tricentric design and a test of a full size 12 inch production valve. The data obtained in these tests provide a substantial base for predicting aerodynamic torques in full size production valves under various operating conditions.
I L
em l
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5.1 Model Tests In 1980, Clow established a program to determine mass flow and aerodynamic torques of the Tricentric design. Exact scale models (see Table 5 ) were designed and built of 150 lb class Tricentric valves of standard design. Scale models of a 12, 24, 48, and 96 inch valve were constructed and tested using University of Illinois facilities under the direction of A.L. Addy, Ph. D. (Engineering Consultant in Fluid Dynamics and Engineering and Associate Head, Department of Mechanical and Industrial Engineering, U. of I. at Urbana Champaign,111.).
The tests were made with air in accord with ISA standards for a straight pipe run flow test. The tests were run at various pressure ratios (upstream to downstream pressure) in both the choked and non-choked pressure regimes. Very low pressure ratios were also applied to allow correlation to incompressible (liquid) flow in accord with ISA standards. Tests were made with flow in the normal direction for Tricentrics (shaft upstream) and for reverse flow (shaft downstream). Further, several
^
pressure ratios near the choked flow point were applied to I
determine the point of choking. This test pointed out that the 1
standard rule of thumb (downstream pressure / upstream pressure =
.523) for determining when choking occurs is not valid at all i
I The tests showed choking will occur at a ratio disc angles.
of.75 in the full open position and.54 in.the near closed j
m M
SMD
" - - - - ~ - - - - _ - - _ _ _ _ _ _ _
position. The test also showed, that although' choking prevents the fluid velocity from increasing, aerodynamic torque will rise in a linear fashion in accord with the pressure differential
{
across the valve in the choked flow regimes.
The models used for testing were made in accord with the
)
Tricentric standard 150 lb cl' ass double flange design. This is a fabricated design in which the seat is at a 10 degree s
angle from a normal to the pipeline axis. Due to the seat 0 from closed to full open.
position, this valve rotates only 80 The valves supplied for the subject job uses a similar geometry d
except the seat is normal to the pipeline axis making this a 900 (k turn) valve design. Therefore, at small opening angles (0 to 200) there are some differences in torque. For angles 0
over this amount, the aerodynamics are the same. Also, at I
small angles the torque approaches the value of the pressure area torque (as explained in Section 2.1.3) thus, differences between the two designs are not significant. With reasonable similarity between the test models and the full size valves.
the data may be used to predict torque characteristics the I
subject valves.
From the data base developed by the model tests a computer i
i program CVAP (Clow Valve Analysis Program) was written for use in predicting valve operating characteristics.
In this program, mass flow rates are predicted by standard e~quations for flow l
I_
h r
(
through an ideal converging nozzle adjusted with coefficients developed in the tests. Torques are predicted on the basis of the equation.
3
{
T=CT a P Dy where
{
T = predicted aercdynamic torque (in Ib)
CT = torque coefficient developed in model tests k-2 AP = pressure differential across the valve (Ib/in )
Dy = nominal valve diameter (in.)
The test performed on a full size 12" valve showed that the mass flow obtained was within approximately 103 of that predicted by the computer model while torques were much less than predicted.
Torques were on the order of 655 of that predicted which could be correlated by changing the power of 3 to 2.84 in the above equation. The power of 3 used in the equation and in the Program CVAP is a derived value obtained by use of the equations for conservation of momentum for a general control volume.
Thus the program indicates torques which would be higher than those obtained in the actual situation.
1 Table 5 shows the dimension of critical (to torque
~
conditions) ele,ents of the double flange Tricentric 12, 24, 48, and 96 inch designs and their scaled down dimensions which I
were used for model construction. Table 6 shows a comparison between the provided size valves and the interpolated sizes.
m
Linear interpolation was used to predict torque characteristics in Clow Program CVAP, thus a similar interpolation of sizes is applicable for size comparison purposes.
It can be seen in the table that very good (less than 10% deviation) correlation was I
obtained for torque critical items. Thus torque data from the program is valid for this application.
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TABLE 5 f
L Test Valve Scaled Sizes (Critical Elements)
VALVE SIZE
{
ELEMENT 12" 24" 48" 96" Full Model Full Model Full Model Full Model i
Size Size Size Size Size Size Size Size I.D.
11.94 3.07 22.62 3.07 46.00 3.07 96.00 3.07 A2 11.33 2.91 21.89 2.97 45.59 3.04 96.20 3.07 K2 10.80 2.78 20.86 2.83 43.44 2.90 91.66 2.93 Shaft Dia.
2.25
.58 3.25
.44 6.0 40 12.0
.38 Shaft CL to l
Seal q., L 2.0
.51 2.69
.36 5.06
.34 7.51
.24 Domed i
Shape Disc Thickness 1.5
.38 1.88
.25 3.75
.25 11.63
.37 Shaft Offset E + 1.2:
.32
.81
.11 1.31
.09 1.18
.04 Shaft Offset LC + 1.67
.43 1.38
.19 2.31
.15 1.66
.05 Ear Width
- 2.25
.58 3.25
.44 6.0
.40 12.0
.38 Ear f
Height
- 3.38
.87 4.88
.66 9.0
.60 15.25
.49
- + E is offset from disc centerline, LC is offset from body centerline t
- Ear is element welded to disc which shaft is mated to.
t Note: Full size dimensions are for a Clou Tricentric 150 lb class double flange design.
u A2 = fiajor axis of elliptical seal
~~
o K2 = Minor axis of elliptical seal E = Offset between shaft axis and disc center (see Figure 2) i LC = Offset between shaft axis and pipe run centarline l
All dimensions in inches i
L TABLE 6 h
Comparison of Production Valve to Valve Model Sizes (Critical Elements)
VALVE
[
_ELEMEllTS l
8" Size Ratio f
- I.D.
7.981 1.05
- A2 7.244 1.09
- K2 7.069 1.07 Shaft Dia.
1.50 1.05
[-
Shaft Q. to Seal Q.,L 1.50
.93
- Disc i
Thickness 1.25
.95 L
[
- Shaft Offset E 1.375 1.05 Shaft Offset LC 1.410 NA Ear Width 2.00 NA Ear Height 5.937 NA 1
~
- Elements considered important to torque characteristics I
fl0TE:
RATIO =
procuction valve size i
A7 = ilajor axis of ciliptical seal t
K = !!inor axis of elliptical seal
= Offse; between shaft axis and disc center (see Figure 2)
LC = Offset between shaf t axis anc Dipe run cent?rline l__
All dimensions in inches
= -
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i
I 5.1.2 Tests sith An Upstream Elbow f
One element of piping system which has an effect on the i
aerodynamic torque of butterfly valves is a turn which may j
occur with an elbow or a tee. Since numerous types of elbows
(
(short and long radius, reducing, mitered, etc.) may exist in a particular piping system, it was necessary to determine a worst case condition for testing. It was determined use of a mitered elbow would be a worst case and that this configu-ration had applicability to flow through tees also.
The mitered elbow produces the greatest separated flow region at the inside of the turn and biases the flow to the outside corner to a maximum. Flow around the corner produces a lower local pressura around the inside of the turn and higher local pressure to the outside. This will oppose closure for geometry 1 (see Figure 12 ) and aid closure for geometry 2 when the disc is in the full open position.
Based on these considerations, models of a 12", 24", and 48" valve (per Table 5) were tested for torque characteristics.
All valve models were tested for geometries 1, 2, and 3 at 2 diameters, downstream from the mitered elbow.
In addition, the The test 12" model was tested at 4 and 8 diameters downstream.
-showed the greatest variation of torque from that obtained for t
)
I--
straight-line flow occurred at 2 diameters downstream from the Differences due to valve orientation were small at 4 i
elbow.
diameters downstream and were just detectable at 8 diameters downstream.
1
For the subject job. valves are installed 10 diameters or l
more from an elbow during LOCA conditions.
Further, the pipe for a
the installed configuration is tapered from a 20" diameter to an 8" diameter pipeline by means of a concentric reducer installed just before the valve. Thus, any turbulance upstream that may affect the torque characteristics of the unit will be eliminated by the flow converging thru the reducer. (See Figure 13 )
Using a straight line pipe configuration to model the valves in the as-installed configuration, then, would be considered a good model.
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Geometry 1
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e Shaft Q, o = 00 Shown Flow FIGURE 12-Valve Orientations P. elative to Upstream Elbow
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Figure 13 The l'.i'jh pret;ure.alvts,Odels with a ccnvergent I
cntrance ;cc-icn 2nc a vahe-disk openine;-angle cr c.0.
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5.1.3 Downstreas Piping Effects 1
s In various tests described in this section, it was necessary In the to provide downstream piping to discharge the flow.
r 1
conduct of these tests the effects of doinstream piping were noted several times. In the straight line\\ tests, a downstream valve was installed to vary back pressure. Any increase in back i
pressure lowered the torque values. In the elboa tests an elbow was installed 20 or more diameters downstream. It showed that for the 24" and 48" models in the full open position, the down-stream piping would choke before the valve model. This prevented any substantial increase in pressure differential across the valve model even with large increases in upstream pressure, thus the torque was limited.
From the piping layouts provided down-stream, piping would provide some degree of back pressure making the assumption of atmospheric pressure downstream used for calcu-lation of torques conservative.
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~ - - - - - - - _ - _ _ _ _ _ _ _ _
Page 56 J
f 5.2 Model Data Verification A test of a full size 12" valve was run at Vought's High Speed Wind Tunnel in Dallas, Texas (see reference 7.08-1) to demonstrate operability and substantiate model test data.
The tests demonstrated the valve would operate in the required 5 second period.
It further showed that torque values were f
less than predicted from model data. The valve used for the test incorporated a one piece thru shaft design while the model had a two piece shaft. To verify the torque effect due to this change, another test was made (data not put into a formal report form) in which a 2 piece shaft was installed in place of the f
thru shaft. The test was made with the disc held in a station-ary position by a manual worm gear type actuator. The result was that the peak torque was the same for both the one and two piece shaft design. The only difference was that the two piece shaft design showed a peak torque closer (by 5 to 10 degrees) to the full open position. A test was also run with the one piece shaft design with the disc held in a stationary position. This was t
done to provide direct correlation with the model tests which were done in this manner.
It also allowed a comparison to the torques measured during the dynamic test with the shaft connected to the pneumatic actuator. A summary of the operability test is included in Appendix B.
~
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M
t 5.3. Application of Model Aerodynamic Test To Full Size Valve Operability Valve Operating Times Expected In Service 5.3.1 All valves are designed to close within 5 seconds for flow I
conditions produced by the maximum differential pressure of 56 PSIG The valves when 100 PSIG is released from the actuator air cylinder.
will close under these installed conditions due to the fact tha i
operator output torque (spring torque) and the valve aerodynamic torque are tending to clost the valve at all disc angles for LOCA and Tables 10 & 11.) While not required for conditions. (See Table 2 LOCA, to open the valve under the above conditions,6120 in-1b of torque is required to crack the disc off the seat, and 5556 in-lb max is required to hold the valve disc open. (See Table 7 _)
The air torque of the actuator (valve open direction) is rated j
l at 9055 in-lb 9 80 PSIG and therefore is more than adequate for the required worst case operating conditions.
7.0-B
) closing times In the Vought Test (Reference The were shown to improve slightly with flow through the valve.
~
l conduct of the test would suggest that opening times in actua service might be re,tarded about.3 to.5 seconds and closing times o
I; might be. improved by the same amount under maximum differential pressure conditions relative to the Clow banch test data.
3
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h Em y.-
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,,-y-y-y,,
w,.
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,,_-.,,_.,,_-,-,,,,vy..,,,,,,w g-,.,,,,
,,-,,.-,,,,,,-.---.-.,..m-7..
5.3.2 Aerodynamic Torques And Mass Flow Rates For Valves As-Installed As described in Section 5.1, torques from straight line model 3 scaling.
tests can be used to predict full size valve torques by 0 Tables 7 thru 9 present torque and other data for the subject valves at various operating conditions. The item of concern for valve operability is TQ (for normal operating conditions, open cycle) and TQA (for maximum operating conditions, closing cycle).
The meanings All positive torque values tend to close the valve.
of the other listings can be found in 7.0 Reference C-1.
To obtain torque conditions for the as installed valves a judgement must be made as to what set of test data most nearly represents the actual conditions. The eight valves for this job are installed in series pairs approximately 2 pipe diameters apart with the shaft side of the units facing upstream into the postulated LOCA flow.
Model test simulating this two valve in series configuration, as well as single valve tests, were run to determine the aero-dynamic torque and mass flow rates for incompressible flow in straight pipeline. (See Reference 7.0. C-2) The applicable con-clusions that can be drawn from these model tests are:
Tne aerodynamic torque coefficient (see Reference 7.0. C-2 1.
for definition of this term) for the downstream test valve was a maximum when the upstream test valve was fully This open and produced the least obstruction to flow.
maximum was less than the maximum torque coefficient of similar single test valve experiments.
M
I The torque coefficient on the downstream test valve became 1
2.
)
independent of the back pressure ratio as the upstream
/
valve-disc approached the fully closed position and was relatively constant near zero for the experiments in which the downstream valve-disc opening angle was larger than the upstream valve-disc opening angle. The pressure distribution on the downstream valve-disc approached a constant value.
The torque coefficients for the upstream and downstream 3.
test valves were generally independent of the spacing between the test valves and the relative orientation.
The torque coefficient on the upstrLam test valve became 4.
relatively constant and nearly zero as the downstream test valve approached the fully closed position for experiments in which the upstream valve-disc opening angle was sub-stantially greater than the downstream valve-disc opening angle.
A modified torque coefficient was utilized for the up-f 5.
stream test valve based upon a local characteriitic pressure drop and was found to be nearly the same as the single test r*
s valve torque coefficient for corresponding valve-disc open-ing angles.and back pressure ratios.
I
)
The maximum value of the torque coefficient for either the 6.
upstream or the downstream test valve was always less than u
the maximum value determined for the single test valve case at the same back pressure ratio.
L
7.
The mass flowrate coefficient far the single test valve experiments increased as the back pressure ratio or valve-disc opening angle increased, since each decreased the losses due to the expansion process.
8.
The mass flowrate coefficient for the two test valves in series experiments was similar to the single test valve values for the cases in which the valve-disc opening angle for the single test valve was equal to the lesser of the valve-disc opening angles for the two test valves in series.
U 9.
An upstream valve-disc opening angle greater than 40 resulted in mass flowrate coefficients for the two test valves in series experiments which were consistently less l
than the corresponding single test valve values.
- 10. The mass flowrate coefficient of the single test valve experiments was improved by the addition of the second test valve in those cases where the upstream valve-disc opening angle was less than 40, probably due to a change 0
~
in the effective flow area related to the expansion processes.
- 11. Over,all, the static pressure drop across the test section has more of an influent e on the mass flowrate through the test section than on the aerodynamic torque on the valve
~
discs.
i
- 12. The test valve spacing and orientation were found to have negligible effects upon the mass flowrate coefficients for the two test valves in series experiments.
m
The performance of the two test valve system generally was 13.
strongly dependent upon the lesser of the two valve-disc opening angles; thus if the two test valves in series were operated independently, the control of the flow would transfer between the two test valves.
Immediate reduction of the mass flowrate, if desired, 14.
would be achieved by operating the system such that the downstream test valve approached the ruliy closed position in advance of the upstream test valve.
If a minimum torque was desired on both test valves during 15.
the closing process, then the two test valves should be closed simultaneously.
Although the experiments which investigated the torque char-acteristics of the upstream test valve were limited, the results were expected to be similar to the torque characteristics of the single test valve experiments which operated under a variable back The presence of the downstream test valve was pressure ratio.
expected to influence the performance of the upstream test valve by altering the back pressure into which the upstream test valve l
The torque coefficients for the upstream test valve as b
l exhausts.
a function of the downstream valve-disc opening angle were run (see Reference 7.0 C-2
).
The results include various upstream
)
valve-disc opening angles (al = 40, 60, and 800), a back pressure 0
0 f
The torque ratio of 0.33, and test valve spacings of 2D and 40.
\\
' coefficients for the upstream test valve for all of the experiments b
(
were equal or less than the corresponding values for the single i
test valve experiments.
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Page 62 c
<1 In two of the as-installed pair of valves, a tee is piped in between. The tee branch is a 4 inch diameter connection used for nitrogen purging and the other ends are 8 inches in diameter for f
mounting into the piping. From information provided by the Bechtel Corporation, this 4 inch line will not be used during LOCA con-ditions. While the 4 inch branch will provide a static blocked off opening in the main 8 inch pipeline, no adverse affects on either the flow or the torque should occur as a result of this opening.
In light of the above considerations, then,using the torque coefficients for a single valve in a straight pipe run will be conservative since the maximum value of the torque coefficent for either the upstream or downstream valve in series is always less f
than the maximum value determined for the single test valve case at the same back pressure ratio.
The mass flow rate calculated for a single valve in a straight pipe run will also be valid because the calculations will be based on the valve disc opening angle equal to'the lesser of the valve disc opening angles for the two valves in series. The test valve spacing and orientation were found to have negligible effects upon the mass flow rate coefficients for the two test valve in series experiments. For the normal operating pressure of 1.5 PSID, any adverse torque or mass flow effects due to the valves being paired
~
in series are at worst negligible because the tests were con-ducted at a much higher.iP.
~
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Tables 10 and 11 shcw model test valve angle and actual valve 0
angle for the supplied units vs torque. There is a 10 difference i
between these due to the seat angle design differences explained in previous sections.
It is reasonable to expect all angles over 20 to be a proper representation of the magnitude and direction of 0
torques. At 20 or below, the magnitudes may differ but the 0
direction is correctly indicated. Since peak torques occur in the 60 to 80 range, these low end torques are of no consequence.
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FLOM
~'
~
t i
c 1%
- o ?g-
_ -, n 9
T.
u %_
,- --f.
-=-n
- ;: W. ---e_M_..._,e:&.- [ 2.,., ;-:,-. --A7 ;%_,v- -
=:
. O - m
'C EW::::..::.T,_'M"-E.'.. n.
j i
a e b h -w h r
=,,_
4
& --~ g =. e g ;,,
i T
Single test valve water table experirrants with a valve-disk
.t opening angle of 80* and a back pressure ratio of 0.45.
l Figure 14 i
f s.
'^
p---
- - ~.. = :::
g-j-
g---
g-l i
1 l
f b
su 3
= ~ ~771- - > 2
=- -
- ::=:m" yt: :Tg-l
~
mg ~.
l
_k i
b f.f
['
t FLou
(
f j N:
\\
I j
l j
?
I b
I
- & ;. & l % ~ c
&%%F#8BaTRWER9f4MRIF31 opening angle of 20* and a back pressure ratio o Figure 15 I
l
i 1
h
- -,- r. w. _
i w,
-..;ge. =..-.= - _ ~ ww-. - -
-_n
..c mgr, _ e=.
= < +. _.. -MDDQ s
b, d
IN N
N g*g 4h- -
'_ ~- av~~# ?.,,. in ci. r: -
FLOW
~
3-
-~
s, -..' -3 5-tt M*
. mWL'~
htSW-.=
.W Mt W 5 E [ $ N.,7.4:.*=.-~ % =Y W-Main!.1%W M
/
Figure 16 Two test valve water table experiments with an upstream valve-disk opening angle of 80, a downstream valve-disk opening angle of 80', Orientation 1, and a back pressure ratio of 0.45.
t i.
P
f~
K92 W.= M a guenw w w % -W7_i?:&
g..C h g, M...r g %.= x m e t n - e _. N T ' W.
m 5' iLTh p % w gM M M_ % T M '
SNbM%
bdk L
FLOW f.5 d.'W Q w s*b ' kg., N7 N. me: e -a N N-N 7 h=- y -
k IEN'&%
h.sb I
CSf3I5$WNf N N 'k N~4 Y Yd 4 N M -.
m
['n f.'
I ii
~
- i 1-l Two test valve water table experiments with an upstream-Figure 17 valve-oisk ocening angle of 80', a downstream valve-disk
_i opening angle of 60', Orientation 1, and a back pressure d
ratio of 0.45.
}
- -a 1
W
mp.
w r
h e
}
jdhi6ic-ww-giEaB
_ _- _ _.ww I
=
y --
- . k =
- c
- ~;
g3gy.y-L-p t
-my w mJ n, M'_%y*W&
W.. '.
22 cm-_.
m E-M v.
w~
N
=s.,, 2 n : - -
?
l
=- w -
=_
b b
Figure 18 Two test valve water table experiments with an opening angle of 60", Orientation 1, and a back pressure ratio of 0.45.
.j L'
l r
kl L,
!l l.,
l II i
l e
i
.i._,
f j
1
- i Page 68
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.M-W i.st.& Ww h M M CQGQ W1MTMXQk '; *=
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+
' l
( 3
. Two test valve water table experiments with an upstream Figure 19
[i valve-disk opening angle of 40*, a downstream valve-disk r
opening angle of 80*, Orientation 1, and a back pressure
[j ratio of 0.45.
'j 4
(
1 e sc 4 # h h M EF P_Z 9 @ M = -- C R i 8 1 1-1 wc_mg._
i- - -=, +- w: s- _=__<__
- A W.,.m
-,?---
g p-
--m-
- g.-f m'.,_
~- 7=1~r_n.L____=
27 ~_ mzw y
,_ g, 4
- m" m y
4 m _ =- @- = m.,2 <c. w _m
- ~
c w~~~"
s
"'" S K d
(, FLOW q-(
g m
W.=: h 4 X'M.
A-L7- %-.AM N2bYh%_--
i S N 'F t'
l Two test valve water table experiments with an upstream Figure 20 valve-disk opening angle of 40*, a downstream valve-disk i
J opening angle of 60*, Orientation 1. and a back pressure
, - ;.(
ratio of 0.45.
sa i
wb%
ish R
t l
i i
,$Le f
I A==
CHARAC CA5E: IECHTEL PILGRIll Ei'ERGD CY F.CW
'3!'TS SYSTI!!: ES VATE: 11-10-33 2 HAFT U3 PATM:
14.70(:SIA)
PSU =
70.70(PSIA)
TSU = S0?.67('t)
DEDIUM: CAS = A GAMA = 1.40
!4W = 29.0 FLOW = ~r GPTION = 2 DV a G.000(IM)
CUTPUT SATA Ci20 KING FOES 3URE RATIOS: PSC/FOU =.749 DFS/?SU =
.198 SOLUTION: Wa0 =
34.42(LIM /S)
T3 EASED ON DIFFERENTIAL PRESSURE AT ONSET OF CMD:GD FLOU NOTE:
TQA PASED ON FSU U? STREAM AND PATM DOL'idSTREAri PSD/?OU =
.743*
ALFHA CF WR DPS/PSU PSU/POV PSC/POU ?0D/FOU TOR 1 30.0.5162 1.0000
.1979
.9327
.7491
.9620.0264 75.0.5066.9314
.2002
.9353
.7864
.6512.1262 70.0.4373.9444
.2046
.9405
.7431
.8394.1543 65.0 4604
.291*
.2103
.9e73
.7374
.B272.1737 40.0 4244.6214
.2165
.7552
.7294 '.8149.1842 55.0.2977.7310
.2235
.9633
.7193
.8030.1977 50.0.34a0.4692
.2293
.971?
.7056
.7918.13 6 *.
45.0.2?90.3303
.2354
.c734
.4897
.7816.1301 40.0.2539.4917
.2405
.9546
.6715
.7726.1712 35.0.2095. /.07 6
.2442
.99?7
.4514
.7651.160s 30.0.1649.3193
.2471
.9926
.6301
.75?O.14?7 25.0.1246.2114
.2J92
.9753
.6035
.7543.1376 20.0.0892.172?
.2505
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.5279
.7511.1314 15.0.0401. 164
.2513
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(*N-LLF)
(IN-L*F)
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4
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PIPE RUM ($MFT UP5TREN'll CA3E 3ECH7EL FILCKIM NORMAL FLOU UHT3 SY371H:
~3 PATE: 11-10-53 CHAPT: US
-FATM:
14.70(SSIA)
PSU
- 16.20(PSIA)
TSU = 521.67(R)
.Y.DIU3: CSS = A GA5'.rA = 1.40 MW = 20.0 F Dt = JF 0;TicH = 3 DV =
1.000(Iiu DPS0 a 1.5MPEIO)
CUT *8:T DATA SOLUTION: 230 =
6.65(LBM/S)
PSD/POU =
.3916 ALFFA CF WP.
DPS/PSU FSU/POU PSC/P0U F0D/P0U TQR1 90.0.5162 1.0000
.0926
.9716
.7431
.?340.0750 75.0.5066.7911
.0?3s
.?727
.7454 0263.1310 70.0.4975.?444
.0?55
.9747
.7431
.9195.1537 65.0 4604.5913
.0931
.9775
.7374
.9125.192?
60.0.4266.3254
.1011
.9803
.72?4
.90!S.1?27 55.0.3977.7510
.1042
.9E42
.7192
.3??f.1971 50.0.3449.6632
.1073
.?e73
.7055
.S? i2.1761 45.0.2799.!?05
.1100
.9906
.6397
.CS?5.1903 40.0.25:7
.e**7
.1124
.??23
.4715
.3360. 316 35.0.2024 4006
.1*44
.??55
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.63:4.1711
- 10.0
.iaG.'31?3
.1159
.9972
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.117c,
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. o 15.0.0(01
- 144
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.5244.1371
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. 133
.?999
.5470
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TQ
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(IN-LB~)
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J'J. 'J
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er...~
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w
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J
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c ?...!.
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- b.. P.,
.; J.3.. t.:
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4 )
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.=
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a..'. 4
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3. '.l f
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< 3 7..*.7 s.,J
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l.
TABLE 9 NORf4AL FLOCCHARACTEBI5 TIC 5'60WNSTREAM)nrr. mm 5TRAIGM F (SHAFT
. r L:..,.;s t e... :. i.
t,.b..., 3..R,.9
..,.t..
n
- i..
.,asc:
UMIT'i 5(3T :1e
~C isN: 11.'.0-33 F0TK:
14.7C(?914)
WFTs I1 e5U =
16.20'.*SIA) 750 = 521.67(R)
F.ESIUM: "AS = n CWAe 1.44 ru = 2?.)
. LO'J = F
- oTIDH = 3 DV =
3.000 r. D
- F90 = 1.30(? SIC)
GbW UT DATre i
SOLUTIDH
'J30 =
7.26(LSM/S)'
FSD/?OU =
.S767 fLPHA
.I
'JR DPS/?SU PSU/?OU PSC/POU FOLi*00 TER1 C0.0.5519 1.0000
.0?26
.96c"
.7522
.?21"
.0144
. 523
.9087
.-}632 75.0
.54E'
.9922
.0?20
.?666 70.0.53;?.9655
.0943
.?685
.7507
.3?61.0776 65.0.5063 0174
.0979
.9717
.7464
.88 5.0960 60.0.4709.E531
.1014
.9756
.7396
.8710.0921 753
.1053
.9790
.72?3
.9537
.09"5 55.0.4235 50.0.3310.6:02
. 092
.9342
.7169
.846E.0064 45.0.330c 2957
.1123
.9352
.7007
.9353.0960 40.0.2754.!047
. ~.159 9916
.6213
.3243
.0*41 25.0.227?
ii'
.1154
.9944
.5600
.9139.0925 30.0
.17's
.32:~
.1203
.9966
.6370
.9339.0903 25.0.1341
.9%
.1214
.99911
.6133
.7943.0S72 20.0.0?57.1734
.24
.9990
.5916
.7655.0853
. e-. s.
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c a,..;
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si.
s.e.n.,
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.9593
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5.0
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) C'/
W TO (DIG) t...)
(LP.4/HR)
(IN-LEF)
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i.
r g-g-
r~~
TABLE 11 Tani r 10__
Torque for as installed conditions for valves; Torque for as installed conditions for valves; A0-5036A, A0-50368, A0-5042A, A0-50428.
A0-5035A, A0-50358, A0-5044A, A0-50448.
All torques in in-lb: (Positive torque tends All torques in in-lb: (Positive torque tends to close valve, negative torque tends to open valve.)
to close valve)
MODEL TEST ACTUAL TORQUE FOR MODEL TEST ACTUAL TORQUE FOR VALVE VALVE INSTALLED CONDITION ANGLE ANGLE NORMAL
- MAXIMUM **
INSTALLED.C0!!DITION VA',VE VALVE MAXIMUM **
NORMAL
- ANGLE ANGLE 80 90
-34 2477 CD 90 73 2477 l
70 80 130 4476 70 80
-61 4476 60 70
-79 5410 60 70 164 5410 50 60 177 5555 50 60
-89 5556 40 50
-93 5180 40 50 173 5180 30 40
-93 4572 30 40 158 4572 20 30
-89 4030 20 30 142 4030 3848 10 20 137 3848 10 20
-84 i
- At 1.5 PSID
- At 1.5 PSID
- At 56 PSID
- At 56 PSID i
i
5.3.3 Conclusions Concerning Valve Operability l
For a LOCA condition it can be seen in Tables 10811 that torques o
for the subject valves are positive (closing) torques for all disc positions. For these valves, any flow condition from none to maximum, in combination with the timed bench tests show the valve will close within 5 seconds or less. As shown in Section 5.3.1, the valves will operate in both the open and closed directions under fully developed LOCA parameters.
For the presented data and supplemental test reports, it has been shown that the valves will operate as designed under the prescribed conditions. This has'been shown using the conservative assumption of no credit taken for pressure ramp in containment and no credit taken for back pressure due to downstream piping.
l The critical elements of the valve, except for the dowel pin l
and keys, were shown to be well within code limits for a design seating torque of 9056 in 1b. per the torque data submitted and summarized in Table 2 Torque values to the keys could reach
(
11,032 in.lbs. The keys are sized based on a minimum tensile strength of 85,000 PSI at 350 F (actual tests for typical material show 100.000 PSI yield at room temperature), a shear value of 60%
of tensile and a 3.0 or better safety factor for internal keys (actuator key has 2.5 safety factor).
For the subject valves with i
a shear area of *1.69 sq. in, for the disc keys and 1.125 for the actuator key, the following stress values result.
Ear key stress = 8703 PSI Actuator key = 13.074 PSI m
m
,y._
,,(_..__
y
..,,..., _7,
.,7
The dowel pin is designed only to r;sist shaft ced pressura lead.
The resultant dowel pin stress for 56 PSIG internal valve pressure u
is:
Dowel pin stress = 1135 PSI The dowel pin is made of alloy steel with a minimum tensile strength i
For the shaft the maximum stress for the given of 110,000 PSI.
torque is within code limits (See References 7.0, A1,2) 5.3.4 NRC 21 Questions Clow has pursued an extensive program to demonstrate operability of purge and ' vent valves in accord with NRC Guidelines.
Since every installation is unique, Clow's basic approach is to The following pages use a combination of test and analysis data.
an item by item response to the 21 point (less 2) list of give These responses considerations issued by the NRC to utilities.
include descriptions of such tests. A copy of the NRC questions responded to in this paper is attached (Appendix A).
The aP across the valve is determined from the customer's 1.
spec and/or data sheet. Clow assumes downstream pressure is atmospheric although it may, in fact, be higher.
Dynamic torque coefficients were developed based on scale 2.
models of a 12", 24", 48", and 96" valve. These were shown to bE Conservative by a test of a full scale 12" i
I Further, model tests were performed for an up-valve.
stream mitered elbow for 12", 24", and 48" models and for 2 valves in series using the 24" models.
For actual pro-4 duction valve disc shapes are identical or only W
W
slightly differe:;t. All differenc;s. c1though small. cre fully documented. (Section 5.1. 5.2. 5.3) 3.
Installation effects were accounted for in a11' cases. but down-r stream piping back pressure was not. since this produces a more
,.:i.
. i.'tt :.~ %
conservative calculation. (Section 5.1.3)
"t 4.
Cic,w does not consider containment pressure response profile.
/.$ ?!,$. '
..: I Clow assumes signal may be delayed until full containment
. 4.,i,~,
E r*4 '
pressure is reached then ithe valve will be called upon to
.Q-.f tr O
close. Time lag for equipment response is not considered by N%,Cy.
y.
s Clow since this is the responsibility of the buyer. Clow does however, record test lag time as part of unit bench testing.
.Gl s. -
.i.f: c (Section 1.2.C. 5.3.1. 5.3.3)
'.%1?.h
.y..:
5.
Valve angle and predicted AP for choking across the valve is
.4#' -
-J" presented however due to piping considerations, some degree
[
of question as to their validity to actual operation is present.
l The maximum AP for all angles. (Section 5.3.2) 6.
Codes used, allowed stresses, and predicted stresses are pre-
,'j?.
n. L' sented in the Code Desiga Report and/or Seismic Analysis Report (s).
(
a L..-
Load combinations are described in these reports. The valve c
is analyzed by finite element techniques. (Section 4.0)
I i
s l
~
I N
9
tyage 7pg 9.
Unless indicated to Clow in the customer spec, no back j
pressure is considered. When back pressure requirements i
are specified, Clow considers it and incorporates it as part of the unit bench test.
- 10. Clow to date has not used accumulators for valves used in containment isolation system service.
- 11. NA to Clow design.
- 12. Units are not modified to limit the travel angle, except by actuator stops or limit switch settings. Such settings are made to limit travel of the disc to being parallel with the pipe centerline. Clow's r port shows, from the test data base and bench tests of each unit, that suffi-cient torque is available to close and seat the valve against all flow induced loads. Since Clow's seat / seal design is conical, no special consideratfor.s for low heat temperature is required. (See Section 5.3.1,5.3.2)
- 13. Clow selects operators for each unit with maximum operating torques much larger than that produced by flow interaction with the disc.
(SeeSection5.3.1)
- 14. Not applicable to air operators.
- 15. Not applicable to air operators.
- 16. Not applicable to air operators. Where a manual jack I
screw is provided, the unit is tagged indicating the full disengagement length of the screw. No automatic features are f-provided to insure disengagement. Proper operation is the responsibility of the user.
?*
1_.
e
h Page 77 l
l-5
- 17. The valve, being of all metal construction except for packings, seal laminations, and gaskets, will not degrade f
[
under the required environmental conditions. Metal 6
components are generally accepted in the industry as suitable for the required environmental conditions. Tests
- at both high and low temperatures have been performed by L
Gebruder Adams of Bokum West Germany for the subject
[
seal / seat design. Seismic considerations are covered by both analysis and previous static load tests.
(See
(
Section 1.2, Section 6.0, Section 7.0 A,B).
- 18. All operators and solenoid valves installed by Clow are qualified to appropriate IEEE requirements by testing.
(See Section 2.2.2,2.2.3).
- 19. All tests are summarized in the supplied qualification report and are documented by separate test reports.
((
(See Section 7.0) 7
- 20. Assumptions and the basis for use of analysis combined with test data are presented in the report.
(All Sections)
~
- 21. Clow provides operation and maintenance manuals describing
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required maintenance intervals (typically replacement at i
1 east every 5 years on all elastomers).
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6.0 VALVE SEALING CHARACTERISTICS 6.1 Normal Sealing The following chart shows the sealing ability of the valves as they were shop tested for record. The tests were performed with pressure on the indicated side of the disc and the opposite side open to atmosphere. The normal recommended flow direction for these valves is with pressure on the shaft side, so when pressure is applied to the clamp ring side, it is considered to be the reverse flow direction. During this test, the air under water method was used to indicate leakage.
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LDBTW Table 12 VALVE SEALING CHARACTERISTICS PRESSURIZED SIDE VALVE CLAMP VALVE SIZE 1EST PRESSURE SHAFT RING LEAKAGE MARK NO.
(IN.)
PSIG SIDE SIDE (BUBBLES / MIN) 56 X
0 8-HBS-BF-25 X
0 A0-5035A 8
5 X
X 0
56 X
0 25 X
0 5
0 56 X
0 8-HBB-BF '
25 X
0 A0-50355 8
5 X
0 56 X
0 25 X
0 5
X 0
56 X
.25 8-HBB-BF-25 X
0 A0-5036A 8
5 X
0 56 X
0 25 X
0 5
X 0
56 X
0 8-HBB-B F-25 X
0 A0-5036B 8
5 X
0 56 X
0 25 X
0
{
5 X
0 56 X
0 8-HBB-B F-25 X
0 A0-5042A 8
5 X
0 k
56 X
0 25 X
0 5
X 0
(
56 x
0 8-HBB-BF-25 X
0 A0-50428 8
5 X
0 56 X
0 25 X
1.75 5
Y 0
's 56 x
0 8-HBB-B F-25 X
0 A0-5044B 8
5 X
0
- ii 56 X
0
~
25 X
0 5
x
.25 56 X
0 8-HB B-B F-25 X
0 A0-5044A 8
5 x
0 56 X
0 25 X
0 5
X n
M e,
6.2 Long Tem Sealing The conical seal / seat design of the Tricentric valve in l
r combination with the laminated metal / asbestos seal offers good long term sealing characteristics. When the seal and seat are machined a certain surface finish is obtained. With this finish certain leak rates are obtained during a bench test (see 6.1).
On a microscopic scale these surfaces contain peaks and valleys.
When the disc is seated, these surfaces mate and high local (above yield) stresses are induced at the peaks. The peaks will yield and deform and form a match between the seat and seal.
As the valve is cycled throughout its life, this match tends to This results in improve and a visual seating pattern appears.
improved sealing as the valve ages.
I This has been verified by experience and is documented in the Shell International Cycling Test (Reference 7.0 0-3).
This test was performed by Gebruder Adams of Bochum, West Germany.
Clow's Engineered Products Division produces the Tricentric design under license of Gebruder Adams. The test showed sealing improved continuously up to 41,000 cycl;s, the limit i
of the test.
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6.3 Debris Effects On Sealing A test was performed to determine the effect on sealing capaht11ty of a Tricentric valve if a foreign object became trapped between the seat and seal. As with any valve, if the object is large enough and hard enough and happens to be caught between the sealing surfaces, the valve will fail to close completely and the valve will leak. Leakage will be dependent on the size and shape of the object and open gap size which remains when the valve does not fully close. Since no stand-ards as to debris size exist, the test made determined leakage due to object damage after the object was removed.
For in plant operation this would represent leakage after recycling of the valve if the object was blown out of the way during recycling.
g The object selected was a cooling tray liner used in the petrochemical industry. It's dimensions were approximately
{
1/8" x 1" x 6" and was a filled polyvinyl chloride plastic of 80 shore D hardness. The valve was closed upon this material, opened to remove the material, then closed again to measure leakage. Depending on the applied seating torque, a leakage of.015SdFMto.333SCFMwasmeasured. This test showed the valve could tolerate some large debris and still maintain a 1
relatively low leakage even with a damaged seal (See reference 7.0 0-2. )
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1 6.4 Sealing Under Temperature Variations The Tricentric design has been used successfully for sealing applications from cryogenic to 9000F. The Shell International Cycling Test describes sealing characteristics for a media operating temperature of 8420F when the body reached a temperature of 7160F 6
l The Tricentric conical seal / seat design lends itself k
well to accommodating temperature changes in the body and resultant size variation of the sealing components. Due to j
the torque seating design and some seal flexibility, the valve
(
will self adjust to the small dimensional variations which could be anticipated for the subject valves. Of course, if large thermal gradients (very unlikely from information provided to Clow) existed around the body circumference higher levels of leakage could be expected. Again no standards exist
~
to the knowledge of Clow personnel which could become a basis for prediction or a test of such leakage.
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6 6
3 1.
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7.0 REFERENCES
(con't)
C.
Air Flow Tests prepared by:
A.L. Addy, Ph.D.
i Urbana, Illinois t
(Engineering Consultant in Fluid Dynamics)
Final report on the Clow Valve Analysis Program CVAP 1.
(Oct.1981). Report covers methods of analysis, development of data base from model tests, and set-up of computer program, to predict characteristics of full size valves.
" Aerodynamic Torque And Mass Flow Rate For Compressible 2.
Flow Through Geometrically Similar Scale-Model Clow Valves In Series." (October, 1982)
D.
Other Reports and Information Operating Instructions for Clow Tricentric Wafer Stop 1.
Valve covers installation, maintenance, and operating instructions for 82-2739(N) valves.
Clow Test Report Project No.82-003 " Effects of Foreign 2.
Bodies on Tricentric Sealing" by Robert $ansone.
Shell International Cycling Test (2/6/72) by M. Nijenhuis 3.
(Note: Clow produces Tricentric valves under license of Gebruder Adams of Bochum, West Germany.)
7 E.
Other References Bechtel Power Corp. Design Specification 10394-P-119-1(Q),
')
1.
Rev. O.
"A' Water Table Investigation of Two-Dimensional Models of 2.
The Clow Corporation Tricentric Valve" by Dr. Robert F.
Hurt, Engineering Consultant, Professor of Mechanical Engineering, Bradley University, Peoria, Illinois, 1
Sept. 14, 1979.
"A Parametric Study of A Butterfly Valve Utilizing The 3.
Hydraulic Anology" by Bruce A. Coers Bradley University, 1983.
" Radiation Sensitivity Analysis of Luminated Valve Seals
~
4*
For Clow Corporation." Wyle No. 17629-01 (Jan. 31, 1983)
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7.0 REFERENCES
A.
Seismic Analysis Reports prepared by:
Patel Engineers Huntsville, Alabama The following include stress and frequency analysis for the subject valves:
Technical Report PEI-TR-83-24, Rev. A.
Seismic 1.
Qualification Analysis of Clow 8-Inch Wafer Stop Valve.
Technical Report PEI-TR-833700-1, Addendum to PEI 2.
Technical Report PEI-TR-83-24 covering 8"-HBB-BF-AO-5035A, 5035B. 5036A, 50368, 5042A, 5042B, 5044A, and 50448.
B.
Seismic Qualification Test Reports prepared by:
Vought Corp.
High Speed Wind Tunnel Facility Dallas, Texas i
1.
Report No. 2-59700/1R-52972 " Simultaneous Static Seismic l
Load of Flow Interruption Capability Tests of a 12 Inch Valve for the Clow Corporation" (Dec. 15,1981).
l i
Application of 11.0 g biaxial static load to valve actuator during operation with choked air flow thru the valve.
Patel Report PEI-TR-83-29. Revision A (Aug. 10,1983) 2.
" Seismic Qualification of Clow Wafer Stop Valve Assemblies" including Addendum I and II.
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APPENDIX A i
NUCLEAR REGULATORY PURGE VALVE OPERABILITY GUIDE LINES
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Page A-I v
f BRANCH TECHNICAL POSITION CSS 6-4
- CONTAINMENT PURGING DURING NORMAL PLANT OPERATIONS f
A.
BACKGROUND This branch technical position pertains to system lines which can provide an open path from the containment to the environs during normal plant operation; e.g., the purge and vent lines of the containment purge system. It supplements the position taken in SRP section 6.2.4.
While the containment purge system provides plant operational flexibility, its design must consider the importance of mini-mizing the release of containment atmosphere to the environs following a postulated loss-of-coolant accident. Therefore, plant
)
designs must not rely on its use on a routine basis.
i The need for purging has not always been anticipated in the design of plants, and therefore, design criteria for the contain-ment purge system have not been fully developed. The purging experience at operating plants varies considerably from plant to plant. Some plants do not purge during reactor operation, some purge intermittently for short periods and some purge continuously.
The containment purge system has been used in a variety of ways, for example, to alleviate certain operational problems, t
such as excess air leakage into the containeegt from pneumatic controllers, for reducing the airborne activity within the contain-ment to facilitate personnel access during reactor power operation, o
- Note:
This paper ir retyped for legibility from paper suoplied by HRC.
i O
r and for controlling the containment pressure, temperature and l
relative humidity. However, the purge and vent lines provide an open path from the containment to the environs. Should a LOCA occur during containment purging when the reactor is at power, the calculated accident doses should be within 10 CFR 100 guide-line values.
The sizing of the purge and vent lines in most plants has been based on the need to control the containment atmosphere during refueling operations. This need has resulted in very large lines penetrating the containment (about 42 inches in l
diameter). Since these lines are normally the only ones provided that will permit some degree of control over the containment atmosphere to facilitate personnel access, some plants have L
used them for containment purging during normal plant operation.
e I
Under such conditions, calculated accident doses could be signif-icant. Therefore, the use of these large containment purge and vent lines should be restricted to cold shutdown conditions and refueling cperations.
The design and use of the purge and vent lines should be based on the pre' mise of achieving acceptable calculated offsite radio-logical consequences and assuring that emergency care cooling (ECOS) effectiveness is not degraded by a reduction in the contain-ment pressure.
Purge system designs that are acceptable for use on non-routine basis during normal plant operation can be achieved by m
.e
Page A-3 providing additional purge and vent lines. The size of these lines should be limited such that in the event of a loss-of-coolant accident, assuming the purge and vent valves are open and subsequently close, the radiological consequences calculated in accordance with Regulatory Guides 1.3 and 1.4 would not exceed the 10 CFR 100 guideline values. Also, the maximum ti.me for valve I
closure should not exceed five seconds to assure that the purge
)
and vent valves would be closed before the onset of fuel failures following a LOCA.
~
l The size of the purge and vent lines should be about eight L
inches in diameter for PWR plants.
This line size may be overly
[
conservative from a radiological viewpoint for the tiark III BWR L
{
plants and the HTGR plants because of containment and/or core design features. Therefore, larger line sizes may bc justified.
However, for any proposed line size, the applicant must cemon-strate that the radiological consequences following a loss-of-s coolant accident would be within 10 CFR 100 guideline values.
In summary, the acceptability of a specific line size is a function of the site meteorology, containment design, and radio-u.
logical source term for the reactor type; e.g., BUR, PilR or HTGR.
B.
BRA';CH T~CM'lIC*L POSITIO!!
The system used to purge the containment for the reactor operati:nal codes of power operation, startup. hot stancby and hot shutdcunt f.e., the on-line purge system, should be indecen-dent of the purqe systen used for the reactor operation rodes of cold shut'own and refueling.
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The on-line purge systen should be designed in accordance with the following criteria:
a.
The performance and reliability of the purge system j
(3 isolation valves should be consistent with the oper-ability assurance program outlined in MES Branch Technical Position MEB-2 Pump and Valve Operability Assurance Program.
(Also see SRP Section 3.9.3) The design basis for the valves and actuators should include the buildup of containment pressure for the LOCA break spectrum, and the purge line and vent line flows as a function of time up to and during valve closure.
b.
The number of purge and vent lines that may be used should be limited to one purge line and one vent line.
c.
The size of the purge and vent lines should not exceed about eight inches in diameter unless detailed justifi-cation for larger line sizes is provided.
d.
The containment isolation provisions for the purge system lines should meet the standards appropriate to engineered L
safety features; e.e., quality, redundancy, reliability and other appropriate criteria.
~
e.
The instrumentation and control systems provided to isolate the purge system lines should be independent and actuated by diverse parameters; e.g., containment pressure, safety injection actuation, and containment radiation level.
If energy is required to close the valves, at least t'.vo diverse sources of energy shall be provided, either of which can affect the isolation function, iL i
l f.
Purge system isolation valve closure times, including instrumentation delays, should not exceed five seconds.
g.
Provisions should be made to ensure that isolation valve closure will not be prevented oy debris which could potentially become entrained in the escaping air and steam.
2.
The purge system should not be relied on for temperature and humidity control within the containment.
3.
Provisions should be made to minimize the need for purging of the containment by installing containment atmosphere cleanup systems within the containment.
4.
Provisions should be made for testing the availability of the isolation function and leakage rate of the isolation valves, individually, during reactor operation.
5.
The following analyses should be performed to justify the containment purge system.
An analysis of the radiological consequences of a loss-a.
of-coolant accident. An analysis should be done for a spectrum of break sizes, and the instrumentation and setpoints that will actuate the vent and purge valves
}
closed should be specified. The source term used in the s
radiological calculations should be based on a calcul-ation under the terms of Aopencix K to determine the extent of a failure and the conccmitant release of fission products, and the fission product activity in the primary coolant. A pre-existing iodine spite should I_
d
b.
I be considered in determining primary coolant activity.
The volume of containment in which fission products are mixed should be justified, and the fission products from the above sources should be assumed to be released through the open purge valves during the naximun interval required for valve closure. The radiological consea-uences should be within 10 CFR 100 guideline values.
b.
An analysis which demonstrates the acceptability of the I
provisions made to protect structures and safety-related equipment; e.g., fans, filters and ducting located beyond the purge system isolation valves against loss of function to control the environment created by the escaping air and steam.
c.
An analysis of the reduction in the containnent pressure resulting from the partial loss of containment atmosonere during the accident for ECCS backpressure deternination.
d.
The allowable leak rates of the purge and vent isolation valves should be specified for the spectrum of design basis pressures and flows agcinst uhich the valves must close.
M ese NW H
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GUIDELIl1ES FOR DEM0!1STRATIO!10F OPERABILITY OF PURGE AtiD '!E::T '!AL'!ES
,0PERABILITY In order to establish operability it nust be shown that the valve actuator's torque capability has sufficient margin to over-come or resist the torques and/or forces (i.e., fluid dynanic,
, bearing, seating, friction) that resist closure wnen stroking I
from the initial open position to full seated (bubble tight) in the time limit specified. This should be predicted on the cressure(s) established in the containment following a design basis LOCA.
Considerations which should be addressed in assuring valve design adequacy include:
1 1.
Valve closure rate versus time - i.e., constant rate 8
or other.
l l
2.
Flcw direction through valvc; AP across valve.
f 3.
Single valve closure (inside containment or outside containment valve) or simultaneous closure.
Establish ii worst case.
4.
Containment back pressure effect on closing torque : argins of air operated valve which vent pilot air inside contain-ment.
5.
Adequacy of accumulator -(when used) si:ing and initial charge for valve closure requiremenu.
6.
For valve operators using torque liniting deviccs - are l
the settings of the devices compatible with the torques required to operate the valve during the design basis condition.
i e-
~en-~~
r 7.
The effect of the piping system (turns, branches) up-stream and downstream of all valve installations.
1 8.
The effect of butterfly valve disc and shaft orientation to the fluid mixture egressing frem containment.
DEMOMSTRATION Demonstration of the various aspects of operability of purge and vent valves may be by analysis, bench testing, insitu testing or a combination of these means.
Purge and vent valve structural elements (valve / actuator assembly) must be evaluated to have sufficient stress margins to withstand loads imposed while valve closes during a design basis accident. Torsional shear, shear, bending, tension and conpression h
loads / stresses should be considered. Seismic loadings should be addressed.
L Once valve closure and structural integrity are assured by
[
analysis, testing or a suitable combination, a deternination of the sealing integrity after closure and long term exposure to the containment environment should be evaluated.
Emphasis should be J
directed at the effect of radiation and of the containment spray Ao chemical solutions on seal naterial. Other aspects such as the effect on sealing frem outsice ambient temoeratures and decris
~
t should be c:nsidered.
[
The folicuing ccnsiderations apoly when testing is chosen as a ceans for demonstrating valve operability:
H
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Page ll-?
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Bench Testino A.
Bench testing can be used to demonstrate suitability of the in-service valve by reason of its tracibility in design to a test valve. The following factors should be considered
-{
when qualifying valves through bench testing.
1.
Whether a valve was qualified by testing of an identical valve assembly or by extrapolation of data from a similarly designed valve.
- i 2.
Whether measures were taken to assure that piping up-stream and downstream and valve orientation are siculated.
3.
Whether the following load and environnental facters were considered
- f a.
Simulation of LOCA b.
Seismic loading c.
Temperature soak d.
Radiation exposure e.
Chemical exposure f.
Debris B.
Bench testing of installed valves to demonstrate the suitability of the specific valve to perform its required function during the postulated design basis accident is acceptable.
1.
The factors listed in items A.2 and A.3 should be considered when taking this approach.
In-Situ Testinc i
In-situ testing of purge and vent valves may be perferrec to confirm the suitability of the valve under actual conditions.
emme
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When performing such test, the conditions (loading, environment) to which the valve (s) will be subjected during the test should simulate the design basis accident.
NOTE: Post test valve examination should be performed to establish structural integrity of the key valve / actuator components.
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End CSB 6-4 l
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CLARIFICATIOil 0F SEPT. 27 LETTER TO LICE!; SEES REGARDI!!G sf L
Deli 0tlSTRATIO10F OPERABILITY OF PURGE Arid VElli VALVES P
1.
The aP across the valve is in part predicated on the contain-i ment pressure and gas density conditions. What were the f
containment conditions used to determine the AP's across the valve at the incremental angle positions during the closure cycle?
[
2.
Were the dynamic torque coefficients used for the deter-
~
mination of torques developed, based on data resulting from c
{
actual flow tests conducted on the particular disc shape /
design / size? What was the basis used to predict torques developed in valve sizes different (especially larger valves)
(
than the sizes known to have undergone flow tests?
3.
Were installation effects accounted for in the determination b
of dynamic torques developed? Dynamic torques are kncun to be affected for example, by flow direction through valves with off-set discs, by downstream piping backpressure, by a
shaft orientation relative to elbows, etc. What was the basis l
(test data or other) used to predict dynamic torques for the particular valve installation?
4 When comcaring the containment pressure response profile against the valve cosition at a given instant of time, was 1
the valve closure rate vs. time (i.e. contstant or other) taken into account? For air operated valves equipped.vith spring return operators, h.1s the lag time from the time the
- i:ote:
This pacer is retyped for legibility from paper supelied by
- RC.
w e.
h
.,j Page A-12 if valve receives a signal to the time the valve starts to stroke been accounted for?
(
NOTE: Where a butterfly valve assembly is equipped with spring to close air operators (cylinder, diaphragm, etc.), there f
typically is a lag time from the time the isolation signal is received (solenoid valve usually deenergized) to the time the operator starts to move the valve.
In the case of an air cylinder, the pilot air on the opening side of the cylinder is approximately 90 psig when the valve is open, and the spring force available may not start to move the piston until the air on this opening side is vented (solenoid valve de-energizes) below about 65 psig, thus the lag time.
5.
Provide the necessary information for the table shoan below for valve positions from the initial open position to the seated position (10 increments if practical).
Valve Position
]
(in degrees - 900 Predicted aP Maximum aP L
= full ocen)
(across valve)
(cacaoility) 6.
What Code, standards or other criteria, was the valve designed to? What are the stress allowables (tension, shear, torsion.
l etc.)' used for critical elements such as disc, pins, shaft 1.
yoke, etc. in the valve assenbly? 'lhat load ccmoinations were usec?
t 9.
For those valve asse clies (with air operators) inside contain.
ment, has the contain: ent pressure rise (backpressure) been consicered as to its ef fect on torque margins availaole (to close and seat the valve) fron the actuator? During the closure period, air must be vented from the actuators ocening
k side through the solenoid valve into this backpressure.
Discuss the installed actuator bleed configuration and crovide basis for not considering this backpressure effect a proolem f
on torque margin. Valve assembly using 4 way solenoid valve should especially be reviewed, f
- 10. Where air operated valve assemblies use accumulators as the y
fail-safe feature, describe the accumulator air systen config-uration and its operation. Provide necessary information to show the adequacy ofthe accumulator to stroke the valve i.e.
sizing and operation starting from lower limits of initial air pressure charge. Discuss active electrical comconents t
in the accumulator system, and the basis used to deternine their qualification for the environmental conditions excer-m ienced.
Is the accumulator system seisnically v.esignec?
11.
For valve assemolies requiring a seal pressurization sys em (inflatable main seal) describe the air pressurization system configuration and operation including neans used to determine that valve closure and seal pressurization have taken place.
Discuss active electrical components in this
, system, and the basis used to deternine their qualification for the environmental concition experienced.
Is this system l,,
seisnically designed.
for this type valve, has it been determined that the ' valve travel st::s" (cicted :ositien) are capable of withstan ing the loads imposed at closure during the CBA-LOCA conciti:ns.
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- 12. Describe the modification made to the valve assembly to linit the opening angle. With this modification, is there sufficient torque margin available from the operator to overcome any dynamic torques developed that tend to oppose valve closure, starting from the valve's initial open position? Is there sufficient torque margin available from the operator to fully seat the valve? Consider seating torques required with seats that have been at low ambient temperatures.
- 13. Does the maximum torque developed by the valve during closure exceed the maximum torque rating of the operators? Could this affect operability?
- 14. Has the maximum torque value determined in =12 been found to be compatible with torque limiting settings where applicable?
- 15. Where electric motor operators are used, has the mintm.m avail.
able voltage to the electric operator under both nor al or f
emergency modes been determined and specified to the operator manufacturer, to assure the adequacy of the operator to stroke the valve at DBA conditions with these lower limit voltages available. Does this reduced voltage operation result in any s'ignificant change in stroke timing? Describe the energency mode power source used,
~
s.
- 16. !!her? electric operator units are equipDed with hanca9 eels, w
does their desi;n provide for automatic re-engagenent of tne
~
mater ocerator following the handaheel mode of operJtton?
If not, what steps are taken to preclude the possibility of 1
t_
I the valve being left in the handwheel mode following some maintenance, test etc. type operation.
t
- 17. Describe the tests and/or analysis performed to establish h
the qualification of the valve to perform its intended function
~
under the environmental conditions exposed to during and after I
the DEA following its long term exposure to the normal plant environment.
I
- 18. What basis is used to establish the qualification of the valve, operators, solenoids, valves? How was the valve assembly (valve / operators) seismically qualified (test, analysis, etc.)?
- 19. Where testing was accomplished, describe the type tests per-formed conditions used etc. Tests (where applicable) such as flow tests, aging simulation (thermal, radiation, wear, vibration endurance, seismic) LOCA-DCA environment (radiation, steam, chemeials) should be pointed out.
- 20. Where analysis was used, provide the rationals used to reach
(
the decision that analysis could be used in lieu of testing.
Discuss conditions, assumptions, other test data, handbook data, and classical problems as they may apply.
- 21. Have the preventive maintenance instructions (part replace-ment, lubrication, periodic cycling, etc.) establisned by the manufacturer been reviewed, and are they being followed?
Consideratien should especially be given to elastomeric ccm.
ponents in valve body, operatcrs, solenoids, etc. where this hard..are is installed insido containers.
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I DESCRIPTION OF OPERATIONAL i STS t
OF A 12 INCH CLOW TRICEllTRIC VALVE -
FOR NUCLEAR PURGE SYSTE!! SERVICE J-BY J. E. KRUEGER NUCLEAR VALVE DESIGN ENGlilEER NOVEMBER 30, 1981 O
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APPENDIX B
SUMMARY
OF 12" CLOW TRICE!!TRIC CHOKED FLOW / STATIC SEISMIC OPERABILITY TEST I
1 l
l (Refer to Vought Corp. Report No. 2-59700/1R-52972) l e
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rP Page 3-1 f
INTRODUCTIOil -
A test was performed at Vought Corp., Dallas, Texas, on November 16, 1981, to demonstrate operability of a 12 inch Tricentric valve for flow and load conditions possible in case of a LOCA (Loss of Coolant Accident) in a nuclear plant. The t
test was run with a valve to be used in Jersey Central Power I
and Light's Oyster Creek Plant. The test was performed by Vought personnel under the direction of a Clow Engineer.
Witnesses to the tests included representatives of GPU fluclear of New Jersey and Bechtel of San Francisco.
OBJECTIVE -
The test was performed to demonstrate that the valve would operate under pressure, flow, and loadings simulating operating and seismic conditions possible during a LOCA.
It was also desired that the open to close cycle be demonstrated to occur in less than 5 seconds. A secondary objective was to show aerodynamic torques produced by air flow over the disc were equal or less than those predicted and used in designing the valve and selecting the actuator.
(Predicted torques used in design derived from previous air flow test perfor.ed with 3 inch scale odels.)
t t
TEIT SET-UP -
iy The valve was installed in a straight pipe run with a stagnation enamber up,trean approximately 6 feet. Downstream I'-
3 feet was a diverging no::le to provent downstream pressure 6
f Page 3-2 from exceeding one atmospnere. Upstream of the stagnation chamber there were several servo-controlled valves used to
[
maintain a constant pressure in the chamber. Air to this f
system was suoplied from Vought's 28,000 cubic feet air storage tanks. The tanks were pressurized to 600 psig with the servo-valves used to maintain a pressure of 65 psig at the stagnation chamber upstream of the valve. Hydraulic load cylinders were provided to produce an 11.0 g load in two perpendir.ular directions through the valve actuator center of gravity.
IflSTRU'1EtiTATION -
Numerous measurements were made during the test with those relating directly to valve operation being printed on an oscillographic chart. These measurements were used to verify test parameters were met during the test and to.snitor valve performance. All data was fed through a digitizer and recorced directly on magnetic tape for later study. Measurements were made at a rate of 10 per second. The measurements taken during the demonstration runs were as follows:
1.
Total pressure in the stagnation chamber.
L i
2.
Total temperature in the stagnation chamber.
3.
Total and static pressure upstream of the Clow valve.
4 Total and static pressure downstream of the Clow valve.
5.
Static pressure in the pneumatic actuator cylincer.
6.
Hydraulic pressure to the static load cylinders.
7.
Angle of the disc in the Clow valve.
8.
Torque on the valve drive shaft.
e
Pagg !!-3 vat.VE AND ACTUATOR DESIGN PARA!!ETERS -
The valve tested was designed for a differential operating pressure of 65 psi and combined operating and seismic loads of 11.0 g's.
The seal was of laminated 316 SST and asbestos.
The body design was 150 lb. class per ANSI B16.34 u
l The shaft
{
used for transmitting torque to close and seal the valve was of a 17-4 PH age hardenable stainless steel, heat treated to h
condition H-1100.
The actuator used was a Bettis NT-3163-SR2
(
pneumatic spring return actuator. The actuator was of a fall closed design with the spring supplying the closing and seating torque (Note: Tricentric valves are designed for torque r
L seating). The actuator was qualified for nuclear service.
CC:: DUCT OF TEST -
L The test consisted of applying the static loads to the f
actuator and establishing a 65 psig upstream pressure with the Clow valve closed.
A signal was then initiated to open the valve.
(
The valve then cycled full open against flow and remained open until a signal to close the valve was provided.
The valve then cycled to the closed position and seateo.
During this period data was taken automatically at 10 measurements per second at all senscrs.
This test was repeated 4 additional times at 65 psig
{
and ente at 35 psig. Mote: These upstream pressures produ:cd b
choked (floa at :enic velocity) flow through the valve during the I
valve open perico.
{-
{
(
Page P.-4 RESULTS OF TESTS -
The tests demonstrated the following:
f
~1.
The Clow disc and shaft geometry provides for a positive aerodynamic closing torque for all angles 1
from full open to full closed.
2.
The aerodynamic torque values used for design of the Clow valve are conservative relative to measured
'f torques.
(Design torques were based on previous 3" scale model tests.)
3.
The construction of the valve is rigid in its design such that no binding resulted under an 11.0 g load applied in two directions simultaneously.
4.
The valve will cycle from full open to full closed in less than 5 seconds with any amount of flow from none to the maximum tested (108 lb/sec of air).
Any value of flow above zero tended to cicse the valve faster (the valve closed in 3.6 sec for a no flow condition).
5.
Operator sizing was sufficient to cycle the valve i
I, from full closed to full open in less than 5 seconds for any tested flow rate.
C0!;CLU5IC!i -
Clow has der.onstrated that their nuclear purge valve design can.eet anc exceed typical specifications for this type of service.
It was fursher shown that the valve will function as m
I en
y P
(
required regardless of the LOCA pressure ramp curve (assumes lower pressures upstream at start of valve closure) often used by other valve manufacturers to show operability.
In conjunction with other tests (now in progress) to show opera-bility under many installed piping configurations, Clow valves
(
can allow full open purge function during shutdown for refueling as opposed to the partially open position now allowed by the NRC. Further, it has been shown that the Tricentric can meet tight leak rate requirements with a metal to metal sealing which is more reliable and less costly in maintenance than
{
sealing with elastomers.
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Attachment Noe 2 W
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CLOW CORPORATION ADDENDUM II
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TO PATEL TECHNICAL REPORT PEI-TR-83-29 i
m C0VERING EXTENSION OF SEISMIC QUALIFICATION TO
^
CLOW WAFER STOP VALVE ASSEMBLIES 8" HBB-BF-AO-5035A&B 8" HBB-BF-A0-5036A&B 8" HBB-BF-A0-5042A&B 8" llBBOBF-A0-5044A&B and to N732-SR80 Bettis Actuators used on the subject valves
^
by STEVEN NONDAHL g
Design Engineer-Nuclear Prepared for Bechtel Power Corporation
~
for
~
Boston Edison Pilgrim Station #600 Unit 1 In Accordance with Bechtel Specification 10394-P-119-1(Q) Rev. O F
L Work Performed Under I
Bechtel Purchase Order No. 10394-P-119-1-AC, Rev. 1 IC 2 /9-f.l ii 1 l Il-2 3 -23 oistaisution CLOW CORPORATION
,,,, g,,,,
ENGINEERED PRODUCTS DIVISION WESTMONT. ILLINOIS g,,,,,,,
etisst
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BECHTFL POWER COPOR ATION JO R 10394
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3 SUPPLIER DOCUMENT STATUS STAMP
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, p e,,
g 1 its Worn may proceva.
November 11, 1983 2 C Submit final document. Work may proceed.
f 3 C Revise and resubmit. Work rt.av proceed f
IL tetnic At N
subiect to resolution of mdicated comments.
'l cont svs f
4 C Aevise and resubmit. Work may not proceed.
l urewa% cat S C Permissien to oroceed not recuired 49
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F L-Pago i l
Clow Corp. Addendum II to Patel REPORT fiO.:
Technical Reoort PEI-TR-83-29
(% ()of E PREPARED SY:
{ed i
,t Q
steven Honaani U
Design Engineer-Nuclear A
p APPROVED BY:
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'/y**~no
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James Krueger Manager-Nuclear Engineering I'
Q. A. REVIE'.4:
d, M ' ' <se Victor Pauperad Quality Assurance Manager ORIG!!iAL ISSUE: November 11, 1993
~
s L
F t
REY.
REY.
REY.
CHECKED Q.A.
DESCR;Pil;'t OF CHAtiGES fM.
DATE BY BY BY Afl0 Pt.",E S DC'!!!ED e
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f The subject valve assemblies, manufactured by Clow Corporation, are shown by this addendum and the referenced reports to meet the requirements qf Bechtel Power Corp. Design Specification 10394-P-119-1(Q), Rev. O " Design Specification For Flanged Butterfly Valves for fluclear Service ior the Pilgrim Station flo. 600 Unit flo.1, f
Boston Edison Co."
My review of the above mentioned design specification and l
l l
this addendum allows me to certify to the best of my knowledge that l
the requirements of the specification have been met.
I WM-M
~Tncodore E. Thygesen' ~
Registered Professional Engineer I
State of Illinois Registration flo. 62-34780 e
4 e
M 4
f iii J
ABSTRACT t -
,f This addendum describes the basis for extension of previous qualifications of Clow Stop Valves and Bettis Actuators tested for Job 82-2053(N) (Philadelphia Electric) to Job 82-2739(N)
(Boston Edison).
It includes identification of candidate assemblies, j
actuators, and components, consideration of the parameters necessary for qualification, and a comparison of the supplied equipment to these pa'rameters. The result is that all units for the subject job are qualified in accord.<ith the presented basis.
7
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TABLE OF C0lTEilTS PAGE 1.0 SCOPE 1
2.0 EQUIPf1EllT TO BE SHOWil QUALIFIED 1
f 3.0 QUALIFICATION BASIS 1
3.1 Valve Assemblies 1
3.1.1 Analysis Performed 1
3.2 Actuators and Accessories 2
3.2.1 Qualification Basis 2
3.2.2 Actuator Candidate Qualification 2
3.2.3 Actuator Accessory Qualification 3
1 4.0 REFEREilCES 4
l APPEllDIX A PICTURES AtlD FIGURES A-1 & A-2 i
'M We 6
6
Page I f
l_
1.0 SCOPE i
This addendum presents information detailing similarities between the equipment supplied under Bechtel P.O. No.10394-P-119-1-AC, f
Rev. 1 (Clow Job No. 82-2739(N)) and equipment tested under Bechtel
]
P.O. 8031-P-144, Rev.1 (Clow Job No. 82-2053(N)).
It further provides the basis for extending the previous qualification tests to the subject valves.
I-2.0 EQUIPMEf1T TO BE SHOWN QUALIFIED l
The following Valve Assemblies and Actuators constitute the can-I didates for qualification:
Bechtel Mark ho.
Clow Serial flo.
Bettis Act. Model No.
8" HBB-BF-A0-5035A 82-2739-01(N)-01 N-732-SR80 8" HBB-BF-A0-5035B 82-2739-01(N)-02 N-732-SR80 8" HBB-BF-A0-5036A 82-2739-01(N)-03 N-732-SR80 8" HBB-BF-AO-5036B 82-2739-01(N)-04 N-732-SR80 8" HBB-BF-A0-5042A 82-2739-01(N)-05 N-732-SR80
]
8" HBB-BF-A0-5042B 82-2739-01(N)-06 N-732-SR80 1
8" HBB-BF-AO-50448 82-2739-01(N)-07 N-732-SR80 8" HBB-BF-A0-5044A 82-2739-01(N)-08 N-732-SR80-M3 1
3.0 QUALIFICATION BASIS 3.1 Valve Assemblies Valve assemblies may be qualified by a combination of analysis and testing. Analysis is required to show that the stress
]
levels and frequency response characteristics are within
[.
required code and spec allowed ranges. Testing is required to show operability in accord with Spec 8031-P-144, Rev. 2 q
Appendix 17, Paragraph 2B thru 2D.
3.1.1 Analysis Performed For valve assemblies the following is provided to meet these requirements:
Analysis of the subject valves is covered and stresses and frequency response is shown suitable by a) Generic report, PEI-TR-83-24, Rev. A. " Seismic Qualification Analysis of Clow 8 Inch Wafer Stop
.alve" and b) Site Specific Report PEI-TR-833700-1.
These have been supplied by separate submittal.
L-
[-
l Page g ff Note: The generic report meets requiements of ASME Section III,1980 Edition through Winter 1982.
The
((
site specific report meets ASME Section III,1980 Edition through Winter 1981. The required design code l
I is ASME Section III,1980 Edition with no addenda.
Although the codes specified in the generic and site lj specific report differ from the required design code g
a review of the required addenda show no impact on the analysis method or conclusions.
I In accord with Table C-1 of Appendix 17 of 8031-P-144, Rev. 2, the subject valve size 8" may be qualified by operability testing of a similar valve design in the size range of 6" I
to 12".
Successful testing performed under Bechtel P.O. 8031-P-144-AC of a 6" valve assembly Serial No. 82-2053-02(N)-01 (Tag No. 6-HBB-BF-AO-57-121) and separate tests of a Bettis I
NT312-SR5 actuator qualifies the subject valve assemblies.
Further, although not submitted for Bechtel approval, (tests were performed for another Clow Job) a test performed at Vought, Dallas, Texas, which was witnessed by John Strohm I
of Bechtel further backs up this qualification for an 11.0 g static load and full choked flow condition. Results of this test are covered in Vought Report 2-59700/1R.52972 which
{I is submitted separately for reference.
l 3.2 Actuators and Accessories 3.2.1 Qualification Basis Although Bechtel and qualification codes give no specific basis for generic qualification of actuators, the following requirements are considered reasonable and prudent i,
to the qualified actuator.
1.The candidate actuator shall be of similar construction 2.The candidate shall supply an output torque less than or equal to a qualified actuator.
- 3. Major components of the candidate actuator (spring can, air cylinder) shall have a lower mass, lesser overhang, o'r more rigid construction than the quali-fied actuator.
^
- 4. Accessory mounting allows components to supply their safety-related function even though mounting details may be different than that previously qualified.
3.2.2 Actuator Candidate Qualification The candidate actuators are Bettis Model N732-SR80 and N732-SR80-M3.
These units incorporate a dual air cylinder and a return spring which provides the safety related function.
6
Page 3 1~
The subject units are similar in design to those tested previously,being of a pneumatic spring return design.
One difference between the supplied units and tested units exists. The present updated Bettis design incor-porates a bolt on spring can support in lieu of the weld on type supplied on the larger units previously tested. The bolting is prevented from loosening by using suitable lock washers. Also construction and I
function are suitable to prevent spring can motion when tied in to the pipe run as required.
On this basis design similarity is maintained. (See Picture dl for actual configuration of support).
The torque outputs, weights, and overhangs of the candidate and qualified actuators are presented below Spring Torque (approx.)
Overhang (in)*
I Actuator Model Valve Open Valve Closed Spring Can Air Cylinder Weight (in. lb)
(in. Ib)
(lb) candidate N732-SR80 19,000 9,000 36.88 23.38 397 l
qualified NT-312-SR5 '
13,400 5,800 35.38 17.25 533 qualified NT-820-SR4-S 144,500
,93,000 73.25 27.95 1491
- Length from mounting surface on rigid center housing From the above and actual actuator dimensions it can be seen that tests of the NT-312-SR5 and NT-820-SR4-5 will qualify the N732-SR80 units. Although not presented here, dimensions of the N732-SR80 (spring and air cylinder diameter) would suggest greater stiffness than the qualified units. Thus primary size and design criteria are met and the units are considered qualified.
L-Note that Bettis Report 37274 includes a test of a N732-SR80-M3. Thus the actuator provided for Mark No. 8" HBB-1 BF-A0-5044A is also qualified 3.2.3 Actuator Accessory Qualification Accessories which require separate qualification are the Asco solenoid valve and Namco switches. Both are quali-fied separately by the manufacturer. Model numbers and qualification report numbers are shown below:
Item Model No.
Qual. Report No & Date Asco Solenoid Valve NPL 831664E AQR-67368 Rev. O Nov. 2, 198 Namco Limit Switch EA130-31302 QTR-105 Aug. 28, 19 Namco Limit Switch EA180-32302 QTR-105 Aug. 28, 19 m
i.-
I The mounting configuration of various components differs to some extent from that previously supplied. The changes that have been made were necessitated by l
actuator size and requirements imposed by Clow on Bettis to provide a design for accessory mounting suitable for
[
the required seismic environment. The junction box I
provided is mounted in the same fashion as on units f
previously tested. The filter and regulator are also mounted in a similar. fashion as the tested units. The I
solenoid valve mounting has been changed from mounting on a hex nipple at the end of the air cylinder to mount-ing on a bracket connected to the rigid actuator center housing. Also the flamco switches were fastened on their side rather than their back to the mounting bracket.
This was done to allow a short straight run of flex 1
conduit to the junction box. A corresponding change was made to the switch trip method from a can to a trip pl a te. The trip plate weight is approximately 6 oz.
compared to approximately 80 oz. for the previous cam I
design. The trip plate is securely fastened by two
- 10 SHCS which provides for a rigid ccnnection.
The solenoid valve mounting will provide for a lower j
acceleration at this point as compared to mounting at I
the end of the air cylinder. The air cylinder mounting provides for a greater cantilevered length and higher -
accel era tions. This can be seen in the accelerometer I
response curves in Bettis Qualification Report 37274.
Since the safety related function of the unit is to close, any failure to tubing connections between the solenoid valve and air cylinder w',ll result in performance of this l
function. On this basis accessory mounting is considered qualified in accord with test described in Patel Report PEI-TR-83-29 4.0 REFERE!1CES Report flo./Date Ti tl e Patel-PEI-TR-83-29, Rev. A Seismic Qualification of Clow Wafer Aug. 10, 1983 Stop Valve Assemblies Job fiumber 82-2053 (fi)
Clow-Addendum I to PEI-TR-83-29 Static Load Test and Seismic Aug. 16, 1983 Qualification of Clow Wafer Stop Valve Assemblies Patel-PEI-TR-83-24,Rev.A Seismic Qualification Analysis June 24, 1982 of Clow 8 Inch Wafer Stop Valve m
-9
j_
Page 5
<v REFERENCES (con't)
Report No./Date Title f
Patel-PEI-TR-833700-1/
Seismic Qualification Analysis of Oct. 4, 1983 Clow 8 Inch Wafer Stop Valve Job I-Number 82-2739-(N )- al l Vought-2-59700/1R-52972 Simultaneous Static Load And Flow f
Dec. 15, 1981 Interruption Capability Tests of a 12 Inch Valve For The Clow Corpora tion Bettis-37274 Aug. 12, 1980 Nuclear Qualification Test Report Namco-QTR-105 Qualification of EA130 Series Limit Aug. 28, 1980 Switches I
Asco-AQR67368, Rev.0 Report on Qualification of Autonatic March 2, 1982 Switch Co. (ASCO) Catalog NP-1 Solenoid Valves for Safety-Related Applications In Nuclear Power Generating Stations.
Picture No.
Description 1
Picture of spring can and with bolt on support bracket N-732-SR80 actuator 2
Picture of accessory mounting on N732-SR80 actuator showing filter, regulator, solenoid valve, junction box, and switch mounting.
3 Picture of actuator with accessories mounted on valve Figure No.
Description 1
Excerpt from Bettis Drawing SPC-9153A showing accessory mounting on NT312-SR5 actuator used i
on 82-2053(N) Job 2
Excerpt from Bettis Drawing SPC-93828 showing accessory mounting on N732-SR80 actuator used on 82-2739(N) Job.
D 6
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Attachment No. 3
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DESIGN REPORT DR-82-2739(N)
Rev. A REPORT COVERS DESIGN OF VALVE TAG NOS.
8" HBB-BF-A0-5035A L
8" HBB-BF-A0-5035B 8" HBB-BF-A0-5036A 8" HBB-BF-A0-5036B 8" HBB-BF-A0-5042A 8" HBB-BF-A0-5042B 8" HBB-BF-A0-5044B 8" HBB-BF-A0-5044A by STEVEN M. NONDAHL DATE: October 7, 1983 PREPARED FOR BOSTON EDISON COMPANY
~
PILGRIt1 STATION #600 UNIT 1 P.O. No. 10394-M-119-1-AC, Rev. 1 E
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i REPORT NUMBER:
OR-82-2739(N), Rev. O PREPARED BY:
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APPROVED BY:
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Q.A. REVIEW:
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ORIGINAL ISSUE:
CC[D2d f 463 (REV. 0)
DESCRIPTION OF CHAtlGES REV. NO.
R P,'
DATE REV. BY CHECKED BY 0.A. BY AND PAGES REVISED A
1/3/84 g'my fh
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Page 2
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I.
DESIGN CODE AND SPECIFICATIONS The following codes, standards, and customer specifications were utilized for the design, analysis, and construction of
{
the subject valves as identified in Section II of this document.
A.
Codes and Standards ASME Section III - 1980 Edition ANSI B16.34 - 1980 - Steel Valves IEEE-323-1974 - Standard for Qualifying Class 1E Equipment IEEE-344-1975 - Recommended Practices for Seismic Qualification of Class IE Equipment IEEE-382-1980 - Standard for Qualification of Safety Related Valve Actuators ANSI B16.5 - 1981 - Steel Pipe Flanges and Flanged
{
Fittings B.
Customer Specifications i
10394-P-119-1(Q), Rev. O Design Specification, 9/2/83 8031-P-353, Rev. 4, Adden.1, Butterfly Valves, (6/28/73) 8031-G-5, Rev. 5, Document Requirements, (2/8/80) 8031-G-13. Rev. 8, Supplier Q.A., (6/21/77) 8031-G-18, Rev. 5 Environmental Requirements (6/16/82) 8031-P-358, Rev. O, Dynamic Qualification Act. (12/1/81) 8031-P-359, Rev.1, Air Operators (5/13/82)
P.O. Item 1.47 " General Requirements" replaces 8031-G-1 The above as modified by the clarifications and exemptions stated in Clow to Bechtel letter (Jacobi to Solyan)
{
dated 6/2/83.
g II.
ITEMS COVERED BY DESIGN REPORT
~
This report covers the design of Clow Tricentric Wafer Style k
Butterfly Valves and accessories produced under the following numoers:
CLCW SERIAL l10. (S)
BOSTON EDIS0N SERIAL t10.
(
82-2739-01(N)-01 8" HBB-BF-A0-5035A 82-2739-01(N)-02 8" HBB-BF-A0-5035B 82-2739-01(4)-03 8" HBB-BF-A0-5036A
{
82-2739-01(N)-04 8" HBB-BF-AO-5036B I
82-2739-01(N)-05 8" HBB-BF-A0-5042A 82-2 / 39-Ollii)-06 8" HBB-BF-A0-5042B 82-2739-01(N)-07 8" HBB-BF-AO-5044B f
82-2739-01(N)-08 8" HBB-BF-AO-5044A
Page 3 i
III. DESIGN 00CUMENTS WHICH CONSTITUTE THE VALVE AND ACCESSORY DESIGNS ARE AS FOLLOWS:
(Note:
Numerous purchased items do not have drawings, but are adequately described in the manufacturing bill of materials) 1 A.
Manufacturing Bill of Material for 82-2739-01(N), Rev. C 8" Wafer Valve, R.H.
Prints per above Bill of Material are as follows:
l B/M Item No.
Print No.
Item Descriotion 0
0-0741A Assembly - Valve & Actuator 1
B-4245 Valve Body Machining 1.1 B-4170 Valve Body Rough 1.3 A-5431 Valve Seat 1.10 A-3450C Mounting Plate 2
B-4206 Disc & Seal Assembly 2.1 B-4172 Disc & Ear Assembly 2.2 C-0299 Disc Ear (single) c 2.4 A-5409 Disc Plate
(
3 B-4171 Clamp Ring 4
A-5464A Seal, Laminated 8
B-4173 Cover Plate 11 A-5410 Spacer 12 A-5411 Annular Key 13 A-5497 Bearing 16 B-4247 Thru Shaft 18 A-5413 Parallel Key (ear) 20.1 B-4273 Gland Tube 20.2 B-4176 Gland Flange
{
25 A-5477 Adaptor Plate 27 A-5496 Lantern Ring 33 A-5415 Parallel Key (Actuator)
B/M Item No.
Description Size 5
Hex Head Cap Screw (disc) 3/8-16 UNC x 1"
(
6 Socket Set Screw (disc) 3/8-16 UNC x 1/2" 10 Hex Hd. Cap Screw (cov. plate) 1/2-13 UNC x 1 1/2" 21 Stud (gland assembly) 1/2-13 UNC x 3"
{
22.1 Hex Nut (gland assembly) 1/2-13 UNC 22.2 Jam Nut (gland assembly) 1/2-13 UNC 24 Socket Head Cap Screw 3/4-10 UNC x 2 3/4" L
(act. mounting) 1 28 Socket Head Cap Screw 3/4-10 UNC x 3" (act. mounting) 1
Page 4 B.
Bettis Air Operators:
Item
Description:
- 1. Bettis N732-SR80-5
- 2. Bettis N732-SR80-M3-S (for use on 8"-HBB-BF-A0-5044A only)
IV.
APPLICABLE ITEMS COVERED IN ANALYSIS:
The code states in NCA-1130(a) that the rules..."are applicable only to those components that are designed to provide a pressure retaining or containing barrier." NCA-1130(b) further states "The rules are not intended to be applicable to valve operators, controllers, position indicators, pump impellers, pump drivers, or other accessories and devices, unless they are pressure retaining parts or act as core i
I support structures or component supports." Thus tnis report and supplemental reports cover only those items relating to pressure retention or as specifically requested by purchase order or spec.
l l
A.
For pressure retention the pressure containing parts are:
(1) Valve Body (2) Valve Disc (3) Cover Plate (4) Cover Plate Bolts (5) Gland Flange (5) Gland Studs and First Nut (7) Pipe Plug (for packing leakoff)
(8) Pipe Plug (for "0" Ring leakoff)
B.
Non-pressure retaining accessories requiring analysis for operability are as follows:
(1) Valve Disc Clamp Ring and Bolts (2) Valve Disc Parallel Key (3) Valve Adaptor Plate Bolts attaching the Adaptor Plate to the Valve Body (4) Valve Actuator Attachment Bolts (5) Valve Shaft to Actuator Parallel Key i
(6) Valve Shaft to Ear Dowel Pin 4
(7) Valve Drive Shaft V.
CALCULATION OF STRESSES FOR DESIGN C0!!DITIONS A.
{
For pressure retaining parts, wall thickness is demonstrated as follows:
I
Page 5 i
-s L
(1) a.
For valve body, the required wall thickness is derived from ANSI B16.34 (Per NC 3512.3). The wall thickness j
l is taken from Table 3 of the ANSI B16.34 - 1981 for a t
valve body I.D. of 7.981.
j required wall = Bw =.31" for Class 150
)
actual wall = 1.44" b.
For the thickness between the shaft penetration bore and flange bolt holes NC 3512.3(d) applies and required wall = Sw =.25 x body wall thickness.
Sw =.25 B = (.25)(.31) =.0775" actualthfUknessis.24" l
(2)
The code does not cover thickness requirements for valve discs of the Tricentric design.
The minimum design thickness is established from the following equation:
td =.707 D(
)b D = valve I.D. (larger than disc diameter to be conse'rvative) = 7.981 i
Pw = design working pressure (62) = 75 PSI Sa = code allowed stress (from Section III Appendix, Table I-7.1 for SA516 Gr. 70 plate) = 17500 PSI Thus td = ( 707)(7.981) (75/17,500)b
=.370 = min required thickness The actual thickness specified on design drawing is
.520".
The equation used corresponds to NC 3325.2 (b) l equation (5) where C =.5 (a conservative assumption for the type of disc boundary condition employed).
(3)
Cover plate thickness is analysed by NC 3325.2 (b),
equation (5)
(
t = d(
)
1 k
[
Page 6
.~
where:
d = bolt circle diameter = 3.25 (per Figure NC 3325.1(i))
C = dimensionless factor =.17 P = hydro pressure of body = 450 PSI S = allowable stress per Table I-7.1 = 17,500 PSI thus t = 3.25 (.17 x 450/17,500)h =.215" A nominal cover plate thickness of 5/8" was selected for the detail.
(4)
Stress levels for cover plate bolting are as follows, using methods of Section III, Appendix XI-3220:
Wm1 = min bolt load to keep gaskets seated during operation 2
=.785G P + (2b-GmP)
Wm2 = min required load for gaskets seating
= bnGy G = 2.50 P = 450 (hydro) b =.25 m = 2.75 y = 3700 Thus:
Wm1 = 7067 LBF Wm2 = 7264 LBF Wm2 > WmI, so use Wm2 = 7264 LBF r
2 The root area for 1/2-13 UNC is.1{6 in L
Thus,.126 in2 x 4 bolts =.504 in Bolt stress is then 7264 LBF/.504 in2 = 14,413 PSI The allowable stress for SA193 Gr. B7 bolts is 25,000 PSI I
l
Page 7
,~
(5) The gland flange and studs are not addressed by the code but the following simplified calculations are (6) supplied:
Sha ft 0.D. = 1.5" Packing 0.D. = 2.275 Stud size = 1/2-13 UNC: (root area =.126")
L = load on studs and gland flange L = w/4 (2.2752 - 1.5 )(450 hydro pressure)
I-
= 1034 lb.
V S = stud stress = load L
(# bolts)(stress area)
S = 1034 2052 PSI
=
}
(4)(.126)
Allowed stress = 25,000 PSI I
For flange loading the worst case is assumed with full load concentrated at flange bore center w
l
'o
[-
}
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i h!'P,'/.'l.'
[9.{.'.-l 2C = 8/t = h i
i us -,.l f
l
a -
I l,--
- 3. I.5
=
4%
W = load / inch circum. = 1034/1.885: = 175 lb/in cir.
Ro = 1.885/2 =.942 a = 3.25/2 = 1.625 Ro/a =.942/1.625 =.58
Page 8
~
s From " Formulas For Stress And Strain", by Roark (5th Edition, P. 334, Table 24, Case 1 and la)
Km =.818 (interpolating for R
=.58) o/a M = KmWa = (.818)(175)(1.625) = 233 in=lb Max = MC/I where I = bh3 12 b = 4.25 - (2 x.5625) - 1.885 t
= 1.24 3
I = (1.24)(.5 ) =.013 12 Max = (233)(.25)
= 4481 PSI
.013 Using this simplified approach it can be seen the stress is well below code values.
G9 (7) Pipe plug (for packing leakoff) b (8) Pipe plug (for "0" ring leakoff)
Table NC-3132-1 of Sectior.' III of the Code references f
ANSI B16.11. " Forged Stee-I Fittings, Socket Welding and i
Threaded". The 1980 Edit 13n of this standard states in Table 1 that for 1/8 to a inch threaded plugs and bushings, y
" plugs and bushings are no{ identified by pressure class.
}
They may be used for ratings up through pressure class 6000."
Therefore, these pipe plugs.are more than suitable for the intended service.
B.
Analysis of non-pressure retaining accessories requiring calculations to show operability is as follows:
(2) Valve disc parallel keys and (5) valve shaft to actuator parallel key:
The calculations of parallel key strengths to determine torque to yield in shear are as follows:
i l:
s N_
.f 3-Page 9 s
(2) Can't.
-(5) Valve disc keys (two of them) have dimensions of 3/8" square x 2 1/4" long.
Yield strength is 75,000 PSI. Shear yield = ( 6) tensile yield
= (.6)(75,000)
= 45,000 PSI Shaft radius is.75" = R Key shear area is 3/8" x 2" =.75 in2 2
Load to yield key is.75 in x 45,000 PSI = 33,750 lb.
33,750 lb. x.75" R = 25,300 in-lb = 2,100 ft-lb for one key. For two keys, then 4,200 ft-lb would be required to yield both keys.
The key in the actuator is 3/8 square x 3" long.
In a similar manner as above, 3.200 ft-lb is required to yield actuator key in shear 7 Actuator output torque for valve seating is 756 ft-lb.
(6) Calculation to determine stress level in the valve
(
shaft to ear dowel pin:
Dowel pin size:
3/8" dia, x 1" ig, omm alloy steel, 110,000 min tensile, 24-30 RC
~
Shear bearing area: Approximate by a circular area For a circle, imax = 4/3 t average F = displacing force on shaft = pressure x n/4 (shaft dia) thus F = n (1.512 x 285 PSI x 1.5 = 755 lb 4
(C'IP )
(Hydro) tav = F O'- r/4 (0 = dowel pin dia.)
tmax = 16F
= 16(7551, 3:(DJ-3:t3/3)"
= 9,115 PSI tall =.63all = 66,000 PSI L
thus 9,115 (tmax)< 65,000 PSI (tall) and loading on pin is acceptable.
1 Page 10
.... s
!~
(6)' Con't.
i For' items (1), (3), (4), and (7) of Section IV B of this report, the analysis is covered in report PEI-TR-833700-1 j
t by Patel Engineers. This report constitutes the " Design
' Report" required by the code.
4 1
1 e
S 3
e O
Page 1 of 3 9
January 3, 1984 I
REPLY TO BECHTEL COMMENTS ON DOCUMENT # DR-82-2739(N), REV. O COMMENT #1 I
Design Code & Specifications Refers to Section II - There is no Section II, unless the following Section III isSection II.
Reply: This is an editorial error and will be corrected.
COMMENT #2 III-A Should correctly reference the Valve Drawing D-0741C i
Reply: Correct reference to the valve drawing is reconciled in Addendum I to DR-82-2739(N), Rev. O.
COMMENT #3 V-A (1)a The thickness per ANSI B16.34 is exclusive of the corrosion allowance of 0.080. The drawing shows a body wall o f.380". The design report states actual wall =
1.44".
The above must be reconciled.
Reply: Care must be taken in the interpretation of just what thbse numbers on the drawing are. Drawing D-0741C states that the minimum thickness of the body wall with corrosion allowance is.380".
This is only the minimum.
Due to the nature of the design of the valve, the actual body wall on tne machining drawing comes out to be, conservatively,1.44".
However, minimum body wall with corrosion allowance should be.390" and not.380". This was an error. The arrangement drawing will be changed accordingly.
COMMENT 84 V-A (2) The disc thickness specified on the drawing is.450 inclusive of corrosion allowance. The calculation shows
.520".
The difference between the two must be reconciled.
Reply: The calculation does not show a thickness of.520".
It shows a calculated thickness of.370".
.370" + C.A. is
.450" which is reflected on the arrangement drawing.
The disc is machined at.520" for conservatism. The report is Correct.
e m
Page 2 of 3 COMMENT #4 V-A (3)
For this type of construction C = 0.20 The thickness required:
d/CP t=
+
C.A.
C = 0.20 g
S d = B.C. Diameter 3.25
(.2)(150)
+.080 S = Allowable Stress =
=
17500 17500 PSI
= 3.25 30
+.080 C.A. = Corrosion Allowance 17500
=.134 +.080 P = Design Pressure = 150 PSI
.215" The calculated thickness is correct, but the individual factors in the formula must coincide with those given in the Code.
l Also the drawing shows a cover' plate thickness of.229".
l This must be corrected.
Reply: The calculations listed in the above Bechtel Comment are' incorrect. Figure NC 3325.1(i) clearly shows the correct flange model, and clearly states that C =.17.
Additionally, the design pressure (P) for the valve is not 150 PSI.
The design is Class 150, which implies a cold working pressure of 285 PSI. The calculations in the report further assume hydrotest pressure (1.5 x 285 PSI) for conservatism.
In other words, the calculations in the report are correct.
I However, the minimum cover plate thickness on the drawing will be changed to agree with what is in the report.
A different equation was used to calculate the thickness when the drawing was made. Again, for conservatism, a 5/8" plate thickness was selected for the detail (making min thickr.ess requirements almost academic.)
e
I.
Page 3 of 3 s
I I
COMMENT.#4 g-V-A (6)
In computing the maximum stress I = (1)* (.5)3
=.0104 12 Max S = 191 = (233)(.25) = 5600 PSI I
.0104
- Note that the calculated moment is per inch of circumference.
Reply: In talking with Al Meyers of Bechtel Power, it was pointed out that this comment was meant for information only. No change to the report is reqyf red.
COMMENT:
Delete or amplify upon the final sentence regarding packing friction.
It is argumentative and inconsequential.
(This applies to Page 8 middle of page.)
Reply: Sentence will be deleted.
trk./k Steven M. Nondahl Design Engineer cc:
J. Krueger O
e
g a
I 10 2 A-DISTRIBUTION BECHTEL POWER COPOR ATION JOa10394 C0" SUPPLIER DOCUMENT STATUS STAMP SLJPPL'E' I
I K Worn may proceed.
CLIENT J
t f
2 Submit final document. Work may proceed.
FIELD l
3 C Revise and resubmit. Work may proceed AAcH subsect to resolution of indicated comments.
Crvit 4 C Revise and resubmit. Work may not proceed.
5 C Permission to proceed not reouired.
ELECTRICAL Perrmssion to proceec coes not constitute acceptance or aDDrowmot oes9a eetais, caculaiens, anaivses. test metmocs or mater aes MECHANICAL O(
a weiooed or se ecteo Dv the sucover, ano oces not reueve supoi.et l
from fue comoseance win contractuae oblyations or reitase any PL ANT CSGN 1
(
hoics claceo on tne contract C t's NM
/
'\\
lAlC E
J M
N P JQ RE\\TAED AECCRO
'dF j
- O N
JOB 10394 l
BYd N f2 < n-D ATE f - t.d g-p BECHTEL POWER CO A POR ATIOP.
Se Francisco jo
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L e
1 1
p-MS%mlhE@gn% BS@.2 becs J. L. Carton /'. McBrida w/o
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f A. Tollor
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w/o
(
C.
B.
Hogg w/a
[' ' '
- c. zito w/a Bechtel Power Co~rporation -
J. Cravotto w/o Enmneers-Constructors R. W.
Posse w/a r(
S.
L. Case w/a F.tiv Bea,e street L
K. Jindal w/a san francisco. Cahtornia K. Jue/C. Shelton w/o R.
Raghavan w/a Mani Aaaress. P O Box 3965. San Francisco, CA 91119 f
H.
Phipps w/a November 24 P/lJ82 99 C. McCullar/M. Osborne w/a
~
PIO556 l
JN
_..O U T s
10394-BLE - 1417 Not/ 2 ' .>
Mr. G.
M.
McHugh, Jr.
Deputy Manager - Nuclear Engineering Department JN UUT Boston Edison Company (NUCLEAR) g 25 Braintree Hill Office Park
[
Braintree, Massachusetts 02184
Subject:
Pilgrim Station 600 Unit No. 1 Job 10394, Boston Edison Company Sub 105 - BECo P.O.
62812 Valve Betterment Program f
Reference:
Letter 10394-BLE-1388 dated September 27, 1982
{
Dear Mr. McHugh:
As part of the valve betterment program, we performed an analysis t
-to determine the size of replacement valves for the existing 20" l-valves used in the primary containment purge, vent, and vacuum breaker lines.
Based on this analysis, we recommend that the existing valves be replaced with 8" size butterfly valves.
The analysis was performed to determine the revised operating points for the drywell and torus supply air fans (VSF-205 A & B),
and standby gas treatmen* system exhaust fans (VEX-210 A & B) using 10" and 8" replac alves.
Available fan performance characteristics were t his analysis.
Based on the revised flow rates, the time t
' purge / vent the primary contain-f ment was calculated.
s are shown on Enclosure 1.
Four (4) times the free voli vell and torus (approximately 1 million cubic feet), e 2pdated FSAR, was assumed as the
{
volume of air / gas to t
.ed. shows the fan and system curves ind xpected operating points for fans VSF-205A & B, and VEX 4
& bv ler the two operating modes stated in Enclosure 1.
As requested, we have initiated the paperwork required to release the calculation to BECo.
I 158/4 e
P go Two Bech'( Power Corporation r-L In accordance with Branch Technical Position CSB6-4, Revision 2-(
July 1981, evaluation of radiological consequences will not be requiced for 8" valves.
Our investigation indicates that 8 inch valves are not available I
from other projects which are under construction or have been cancelled.
Therefore, we intend to solicit bids from the following vendors to procure ten (10)-8 inch replacement valves.
Enclosure 3 is the data sheet of the valves we irtend to ask for bids.
- Jamesbury Posi-Seal
- Allis-Chalmers
- Clow Pratt We will forward our recommendation af ter the receipt of bids.
Very truly yours, j
C.
B.
Hogg N {/,
Project Engineer
,CBH:KKJ:RR:jat
Enclosures:
- 1. Calculation Results (Table) 2.
Fan Curves and System Curves
- 3. Valve Data Sheet DPv:n: ((omr!c:en R29f.Y 70 CH2ON N O._
~
P2QUMES REPLY "M m e ZNo Oves Date Due
!dS,"12 3 G_rpen PIO556 156/4 m.
(
Enclosuro(. to BLE- /.f/7 f
f CALCULATION RESULTS MODE 1 SIMULTANEOUS PURGING & VENTING OF DRYWELL AND TORUS 10" Isolation 8"
Isolation Valves Valves Time req'd Time Reg'd Expected Flow to purge /
Expected Flow to purge /
Rate vent Rate vent 3300 cfm l5-1/2 hours 2500 cfm 7-1/2 hours MODE 2 INDIVIDUAL PURGING & VENTING OF DRYWELL AND TORUS
(
10" Isolation 8"
Isolation Valves Valves Time Reg'd Time Reg'd Expected Flow to purge /
Expected Flow to purge /
Rate vent Rate vent 2400 cfm 4 hour4.62963e-5 days <br />0.00111 hours <br />6.613757e-6 weeks <br />1.522e-6 months <br />sts.
1450 cfm 6-3/4 hours Za..
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- n. E.n t.r 14/7
Attachment No. 5 References (Note:
Numbers in parentheses represent Bechtel i
Document No./ Transmittal No. for those documents reviewed by Bechtel)
A.
Seismic Analysis Reports 1.
Technical Report PEI-TR-83-24, Rev. A.
Seismic
{
Qualification Analysis of Clow 8-Inch Wafer Stop Valve.
(10394-M-119-1-13-1/SFP 26663) i 2.
Technical Report PEI-TR-833700-1, Addendum to PEI l
l Technical Report PEI-TR-83-24 covering 8" - HBB-BF-AO-5035A, 5035B, 5036A, 5036B, 5042A, 5042B, 5044A, and 5044B.
(10394-M-119-1-18-1/SFP 37237) 3.
Technical Report PEI-TR-833700-1, Revision A (10394-M-119-1-18-2/SFP 26688)
B.
Seismic Qualification Test Reports
(
1.
Report No. 2-59700/1R-52972 " Simultaneous y
Static Seismic Load of Flow Interruption Capability Tests of a 12 Inch Valve for the Clow Corporation" (December 15, 1981).
Application of 11.0 g biaxial static load to valve actuator during operation with choked air flow through the valve.
(10394-M-119-1-6-1/SFP 26663) 2.
Patel Report PEI-TR-83-29, Revision A (August 10, 1983) " Seismic Qualification h
of Clow Wafer Stop Valve Assemblies"
-including Addendum I and II.
(10394-M-119-1-22-1/SFP 26663) 3.
Bettis-37274, Nuclear Qualification Test Report, August 12, 1980.
(10394-M-119-1-24-1/
SFP 26601) 4.
Namco-QTR-105, Qualification of EA180 Series Limit Switches, Augu'st 28, 1980.
h (10394-M-119-1-30-1/SFP 26663) _ ___
L-f 5.
Asco-AQR67368, Rev. O, Report on Qualification of h
(ASCO) Catalog NP-1 Solenoid Valves for Safety-Related Applications In Nuclear Power Generating Stations, March 2, 1982.
}
(10394-M-119-1-21-1/SFP 26663)
C.
Air Flow Tests 1.
Final report on the Clow Valve Analysis Program CVAP (October 1981).
Report covers methods of analysis, development of
(
data base from model tests, and set-up of computer program to predict characteristics of full size valves.
(10394-M-119-1-12-1/SFP 26601) 2.
" Aerodynamic Torque And Mass Flow Rate for Compressible Flow Through Geometrically Similar Scale-Model Clow Valves in Series."
(October, 1982)
(10394-M-119-1-10-1/SFP 26601) b D.
Other Reports and Information 1.
Operating Instructions for Clow Tricentric Wafer Stop Valve covers installation, maintenance, and operating instructions for 82-2739(N) valves.
(10394-M-119-1-25-1/SFP 26664) 2.
Clow Test Report Projet No.82-003 " Effects f Foreign Bodies on Tricentric Sealing" by Robert Sansone.
l (10394-M-119-1-8-1/SFP 26601) 3.
Shell International Cycling Test (2/6/72) by M.
N Nij enhuis (Note:
CLow produces Tricentric valves
/
under license of Gebrader Adams of Bochum, West Germanv.)
(10394'-M-119-1-50-1/SFP 26688)
E.
Other References l
1.
Bechtel Power Corporation Design Specification 10394-P-il9-1(Q), Rev. O.
2.
"A Water Table Investigation of Two-Dimensional Models
)
of The Clow Corporation Tricentric Valve" by Dr. Robert F. Hurt, Engineering Consultant, Professor of Mechanical Engineering, Bradley University, Peoria, Illinois, 1
September 14, 1979...
l l
"A Parametric Study of A Butterfly Valve Utilizing 0
The Hydraulic Anology" by Bruce A. Coers, Bradley 9
3.
University, 1983.
" Radiation Sensitivity Analy' sis of Laminated Valve Seals for Clow Corporation.
Wyle No. 17629-01 4.
(January 31,1983) /SFP 26601)
(10394-M-119-1-7-1 I
l I
')
)
b.
_ _ - -. _ - -. -. - - -. _ _. _ -. _ _ _.. - _.,