ML20080Q617

Rev 0 to Stress Analysis for Demonstration of Operability of Purge & Vent Valves During Dbas

ML20080Q617
Person / Time
Site:	Oyster Creek
Issue date:	05/21/1981
From:	Shiao A GENERAL PUBLIC UTILITIES CORP.
To:
Shared Package
ML20080Q609	List: ML20080Q607 ML20080Q617
References
PROC-810521, NUDOCS 8402240134
Download: ML20080Q617 (21)

Text

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TDR NO.

l REVISION NO.

O 1302 TECHNICAL DATA REPORT PROJECT NO. PAGE OF PROJECT: Engineering & Design DEPARTMENT /SECTION Oyster Creek Nuclear Station RELEASE DATE 5/21/81 REVISION DATE DOCUMENT TITLE: Stress Analysis for Demonstration of Operability of Purge and Vent Valves During Design Basis Accidents ORIGINATOR SIGNATURE DATE APPROVAL (S) SIGNATURE DATE A. C. Shiau /. C. [4/"8f K. M. Jasani jtNd[f N)mu* 6 MII8I A. P. Rochino h M /

• _ S/u/P/

'W APPgg FORgMNAL DISTRIBUTION DATE

[AXML S-U-91 o DISTRIBUTION ABSTRACT:  !

• R. C. Arnold a. Brief Statement of Problem G. R. Capodanno

• P. R. Clark In accordance with Jim Knubel'sletter to D. K. Croneberger D. K. Croneberger, dated November 11, 1980 D. N. Grace (Reference 6.7), it is requested that the K. M. Jasani analysis be performed to verify that when R. W. Keaten containment purge and vent valves, greater J. Knubel than 3" nominal diameter , are 30* open, J. P. Moore, Jr. these valves will be capable of performing A. P. Rochino their intended function without damage to A.C. Shiau critical valve components during the Design T. E. Tipton Basis Accident - Loss of Coolant Accident R. F. , Wilson (DBA-LOCA) loads and that the valves will close when fluid dynamic torque are introduced.

Per Rober t E. Weltman's letter to John L.

Sullivan, Jr., dated May 16, 1980 (Reference 6.6), the valves to be analyzed are:

1., Drywell Purge Valves V-23-13 and V-23-14 l 2. Torus Purge Valves V-23-15 and V-23-16

3. Torus Vent Valves V-28-17 and V-28-18

4. Drywell Vent Valves V-27-1 and V-27-2

5. Drywell Purge Valves V-27-3 and V-27-4.

The stress analysis results for demon-stration of opetability of purge and vent valves per NRC guidelines dated 9/27/79 (Reference 6.8) are documented in Section 3.0 of this TDR.

8402240134 840221 PDR ADOCK 05000219 PDR p

GCOVER PAGE ONLY Aooo oo3o 9 80

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b. Summary of Key Results

1. The valve operators are able to resist the reaction of LOCA induced fluid dynamic torques (see Table 3 in

. Appendix).

2. The calculated stress levels of the valve components under combined seismic and LOCA conditions are less than LOCA allowable limits of 90% of the yield strength of the material used (see Table 5 in Appendix).

c. Conclusion

1. The fluid dynamic torques tend to close the valve.

2. The structural integrity of the valves is assured if the valve openings are limited to 30' or less.

d. Recommendations

1. To ensure structural integrity, the valve opening must be limited to 30*

open or less.

2. To ensure sealing integrity, the valve

, seats must be visually inspected and be

' replaced as required.

-W e.

IrCII)['ECLCECET .

266 TITLE O. C. - Stress Analysis for DTonstration of Operability PAGE of Purge and Vent Valves Dring Design Basis Accidents 1 OF REV

SUMMARY

OF CHANGE APPROVAL DATE l

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Oyster Creek Nuclear Station Stress Analysis for Demonstration of Operability of Purge and Vent Valves During Design Basis Accidents Table of Contents Title Page Abstract

a. Brief Statement of Problem 1

b. Summary of Key Results la

c. Conclusion la

d. Recommendations la Section 1.0 Purpose and Summary 2 2.0 Methods 4 3.0 Results 7 4.0 Conclusion 8 5.0 Recommendations 9 6.0 References 10 7.0 Appendix 11 9

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f j 1.0 PURPOSE AND

SUMMARY

The purpose of this TDR is to document the results of the analysis for the containment purge and vent valves regarding structural adequacy to withstand the fluid-dynamic torques which would occur during the faulted condition of a loss of coolant accident (LOCA) within the containment vessel and the design basis seismic loads per design specification (Reference 6.4).

According to Reference 6.6, the valves to be analyzed are valves V-23-13 and V-23-14 (Drywell Purge), V-23-15 and V-23-16 (Torus Purge) , V-28-17 and V-28-18 (Torus Vent),

V-27-1 and V-27-2 (Drywell Vent), and V-27-3 and V-27-4 (Drywell Purge).

In summary, the NRC guidelines for demonstration of operability of purge and vent valves dated 9/27/79 (Reference 6.8) has been incorporated in this evaluation.

A. Consiterations Per NRC guidelines (Reference 6.8) the following considerations have been addressed.

1. Valve closure rate is constant per valve manufac-turer's information (Reference 6. 5) . The fluid dynamic effects tend to close the valve.

2. To qualify valves for an opening of 30* or less from the closed position, the maximum differen-tial pressure-across the valve are used in the analysis.

3. Worst case is determined as a single valve closure with the specified maximum differential pressure across the valve per Reference 6.4.

4. Containment back pressure have no effect on closing the valve.

5. The subject valves do not use accumulators.

6. There are no torque limiting devices for the air operated valves for Oyster Creek nuclear station.

7. The effect of upstream piping is ignored as a conservative approach.

8. The valve disc and shaf t orientation does not affect torque calculations.

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e B. Stress Analysis Stress analysis of the valve components under com-bined seismic and LOCA conditions is performed using the design rules for Class 1 valves as detailed in Paragraph NB-3540 of Section III of the ASME Boiler and Pressure Vessel Code (Reference-6.1, hereafter referred to as the Code). The calculated stress levels are compared to code allowables, if possible, or the LOCA allowables of 90% of the yield strength of the material used.

C. Operator Evaluation In evaluating the structural integrity of the valve operators, the calculated torque during LOCA is compared with .the maximum torque rating of the operator per manufactures's data.

D. Sealing Integrity The EPDM seats for valves V-27-1, V-27-2, V-27-3, and V-27-4 have a maximum cumulative radiation resistance of.5 x 107 rads, and the Nitron seats for V-28-17, V-28-18, V-23-13, V-23-14, V-23-15, and V-23-16 have 1 x 105 r' ads per manuf acturer 's information.

Decontamination chemicals have very little effect on these valve seats.

Valves at outside ambient temperature below O'F, if not properly adjusted, may have leakage due to ther-mal contraction of the elastomer, however, during LOCA conditions, the valve internal temperature would be expected to be higher than ambient which tends to increase sealing capability af ter valve closure. The presence of debris or damage to the seats would obvi-

ously impair sealing. To ensure sealing integrity, the seats must be visually inspected and be replaced as required.

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2.0 METHODS This investigation consists of fluid dynamic torque cal-culations, valve stress analysis, and operator evaluation.

2.1 Torcue Calcula tions The method for calculating torques required to operate butterfly valves as described in Reference 6.3 is used in the analysis.

The operator torques are calculated using the following formulas:

T s

= CD g (1)

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T = 4.71 D 2 df op (2).

b 3

Td = CD t A P (3) 4 T

h

= 3.06 D (4) where T = seating torque in ft.-lbs.

s Tb = bearing torque in ft.-lbs.

Td = fluid dynamic torque in f t.-lbs.

T = hydrostatic torque in' f t.-lbs.

h D =. diameter of valve in ft.

d = dianeter of shaft in in.

Ap = pressure drop across valve in psi.

C = coefficient of seating torque s ,

C = coefficient of dynamic torque t

f = bearing friction coefficient = 0.25 The torque coefficients are obtained from the valve manu-facturers. To simplify the calculations, the maximum differential pressures across the valves are conserva-tively used for vacir;a valve opening angles of 0 through 30'.

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The maximum required operating torque for the valve is either a combination of seating and bearing torque or bearing and dynamic torque. Therefore, the maximum torsional loading can be determined from the higher value given by the following formulas:

(To)1 = Tb + Ts + Th (disc in the closed position) (5)

(To) 2 = 1.2 Tb+Td (disc in the open position) (6)

The detailed torque calculations are documented in Reference 6.9.

2.2 Valve Stress Analysis This analysis used the desig'n rules for class 1 valves described in paragraph NB-3540 of Section III of the ASME Boiler and Pressure Vessel Code (Reference 6.1). The requirements for class 1 valves are much more explicit thar for eitner class 2 or 3 design rules. The analysis is conservative since- the design rules for class 2 and 3 valves are exceeded by the rules for class 1 valves.

Valve components are analyzed by hand caculations under the assumption that the valve is either at maximum fluid dynamic torque or seating torque during the LOCA condi-tior.s against the maximum design pressure or the maximum differential pressure across the valve as specified in Reference 6.4. Analysis temperature is 340*F per Refer-ence-6.4. The SSE seismic accelerations are simulta-neously applied in each of three mutually perpendicular directions.

Seismic loads are conservatively taken as 1.5 times of the acceleration levels given in Reference 6.4. The acceleration constants 9xt 9y and 9z represent accelerations in the x,y and z directions respectively.

The coordinate system is defined as the x axis along the pipe axis, the z axis along the shaft axis, and the y axis mutually perpendicular to the x and z axes. Valve orientation with respect to gravity is taken into account by adding an equivalent lg load to the seismic load in the proper direction. The acceleration constants used are summarized in Table 1 in Appendix.

The detailed stress analysis is given in Reference 6.9.

The calculated stress values are compared to code allow-ables, if possible, or LOCA allowables of 90% of the yield strength of the materials used. Code allowable stress levels are Sm for tensile stresses and 0.6 Sm for 5-

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Sm is the design stress intensity value as defined in Appendix I, Table I-1.1 of Section III of the Code. The valve. component materials are listed in Table 2 in Appendix.

2.3 ~Ocerator Evaluation The maximum operating torque for valve due to flow under specified LOCA conditions as calculated in Section 2.1 is used to verify the-structural adequacy of the operator.

The valve operator-structural evaluation is based on a comparison of the calculated maximum torque against the operator ability to resist the reaction of LOCA induced =

fluid dynamic torques per manufacturer's data (Reference 6.5).

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3.0 RESUuTS The results for torque calculations are summar ized in Table 3 in Appendix. The maximum torque absorption capacility cased on manufacturer's advice is also pr e sen ted in the Table. The evaluation shows that the operators are structural.1.y adequate for valve opening angle up to 30* from closed position.

Table 4 in Appendix shows the minimum valve body wall thicknesses versus code required minimum thicknesses.

All the valves satisfy the cinimum wall thickness requirement of the Code.

The calculated stress levels of the main elements of the valves are listed in Table 5 in Appendix. The results indicate that the valve components stresses meet the code allowable stress limits, or the LOCA allowable limits of 90% of the yield strength.

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4.0 CONCLUSION

All ten (10) valves are structually adequate if the valve opening angles are limited to 30* or less from the closed position. This is based on consideration of combined effects of LOCA, pressure load, and DBA seismic loads.

Structural adequacy is assured for the operators and the valve components.

i 5.0 RECOMNENDATIONS l l

1. To ensure ~ structural integrity, the valve openings  !

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must be limited-to 30' open or less from the closed l position. ,

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. 2. . To ensure sealing integrity , the valve seats must be ,

visually inspected and be replaced as required: '

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6.0 REFERENCES

6.1 ASME Boiler and Pressure Vessel Code,Section III, 1980 Edition.

6.2 Steel valves, ANS.I B16. 34-1977.

6.3 AWWA Standard for Rubber-Seated Butterfly Valves,

-ANSI /AWWA C504-80.

6.4 Procurement Specification No. 492-7, Air Operated Butterfly Valves, Non-N Stamped ASME III, Nuclear Safety Related - Class lE, Oyster Creek Nuclear Generating Station, Revision 1, Date 4/8/81.

6.5 Valve, Applicable Data from Manufcturers, A. C.

Shiau letter to A. P. Rochino dated 5/15/81.

6.6 Robert-E. Weltman letter to John L. Sullivan, Jr . ,

dated :4ay 16,1980.

6.7 Jim Knubel letter to D. K. Croneberger dated 11/1/80.

6.8 The NRC Guidelines for Demonstration of Operability

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of Purge and Vent Valves, dated 9/27/79.

6.9 Oys ter Cret - Purge and Vent valve Analysis Calculation 6-.7k, Calculation No. 1302X-322C-A07.

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7.0 APPE:: DIX Tables 1 through 5 are presented in this Appendix.

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TABLE 1 SEIS>1IC IGOS DIi<.u.1'ICK NFRATICM IEEIS T

I F DATICri Shaft Axis is Vertical Shaft axis i.s horizontal Values given Values used Values given values uscd in Reference 6.4 in the k.nlysis in Reference 6.4 in the Analysis gx 3g 4.59 39 4.5g (pipe axis) gy 39 4.5g (3+1)g (4. 5+1)g gz (3+1)g (4. 5+1) g 3g 4.5g (shaft axis) i b

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TNITE 21%TERIAIS FOR VALVE CN.2 VALVE - bWrEIUAIS CCMPCNHfrS Group A (1) Group B (2) Group C (3)

Valves Valves Valves i Dody ASIM-Al26 Class B ASTM-Al26 Class n Carinn Steel - Plate ASIM-A536 SA351 CFHM Ni-resist tb. 2 -

Disc ASIM-A532 17-4 Pil cordi. tion 1075, 316 S.S.

Sluft SA564 Sinft Key ASIM-A582 ASIM-A304, Grade 86-3011 SAE1035 ASIM-B438, Type 2 Teflon Teflon Bushirgs 304 S.S. 17-4 Pil condi. tion 1075, 316 S.S.

i Disc Pins SA56A OI Carbon Steel SAE Grade 2 SAE Grade 2 Operator Bolts l

Note: (1) Group A valves are V-27-1, V-27-2, V-27-3, en d V-27-4, the centerline 18" valves.

(2) Group B valves are V-28-17 and V-28-18, the Fisher Controls 12" valves.

(3) Group C valves are V-23-13, V-23-14, V-23-15, and V-23-16, the Fisher Controls 8" valves.

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L M ,.,abrAdu L1 aihLas i m Lxala VALVE VALVE STRESS STRESS LEVEL ALIGfdlLE dTMS GPGP OCI E CI E fr NAMS AND SYMBOL (PSI) (PSI)-

2423 Sm 9(

Primny Mmbrane Pm Prinnry plus secondary 09 7012 'i Sm 0.9 ff stress due to internal 12600 , 27000 pressure

'i.5 Sm

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pipe Pod 4574 Axial 18900 , 0.9 2700 (d Body reaction -

1.5 Sm 0.9 Cf A stress Bending Peb 16631 18900 , 27000 1.5 Sm- 0.9 af f-27-1, 'Ibrsion Pet 8648 18900 , 27000 7- 2, f-2e-3, 'Ihermal secordary Qt 444 Sm 0.9%

Stress 12600 27000 f-27-4) ,

Prinnry plus Sn 23885 3 Sm 0.9 (y secondary stress 37800 , 27000 Disc -

CaTbined Bending S(l) 4032 0.9 #f L Stress on disc centerline 40500 N

I 5341 Torsional shear Stress S(9) 0.9 uno(d Cmbined Shear stress S(6) 6030 yo Shaft Conbinal bending S(5) 8884 0.9 (y stress 36000 Canbined stress S(4) 11931 0.9%

(shear arxl bending) 36000 Shaft Key Shear stress on S(16) 11664 0.9 (j key 36000 Disc tapper Shear stress in S(17) 23999 0.9 (y pins pins 40500 Bushirns Bearing stress in S(21) 2191 Canpressive allowable (shaf t bearing) bushings 4000 Operator Tension in bolts S(54) 1530 0.9 #f Fbunting +S(55) 51300

~Shear due to S(57) 4308 0.9 (f

, Tontue on bolts 530 3 , ').,0)

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STRESS LEVEL ALIO@ ALE STRESS W1VE VALVE STRESS (XI@ Cr e T NAME AND SNL (PSI) (PSI)-

GPCUP Sm 0.9Oy W anc m 1360 12600 , 27000 Primary plus secondary Op 3825 Sm 0.9 f stress due to internal 12600 , 2700d i

pressure pipe Axial Pcr3 3820 1.5 Sm 0.9 9 18900 27000 Body reaction 1.5 Sm stress Bending Peb 9050 0.9 9 B , 18900 , 27000 7211 1.5 Sm 0.9 r

'Ibraion Pet 18900 . 2700 17, 28-18) ,Ihcrmal secondary Qt 468 Sm 0.99 Stress 12600 , 27000 Primary plus Sn 13237 3 Sm 0.90'y scrondary stress 37800 , 27000 Disc Conbincrl Bending S(l) 2822 Sm Stress on disc centerline 17900 0

Torsional chcar Stress S(9) 9869 0 Coihined Shear stress S(6) 10134 0.6 Sm

.21GDn Shaft Canbincxl bending S(5) Sm stresu 6747 46000 caid;ino.1 streun S (4 ) 14054 an (chear and bending) 46000 Shaft Key Shear stress on S (16)' 21531 0.99 key 90000 Disc tapper Shear stress in S(17) 27483 0.6 Sm pins pins 27600 Uushings Bearing ctress in S(21) 1349 Coupressive allowable (shaft bearing) bushings 10000 Operator Tension in bolts S(54) 27991 0.9%

iS (SS) 51300

. Mauntire Shear due to S(57) 21899

, Torque on_ bolts 0.9r[

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wux 3 (wato; p.TMmR37zos STRESS sucSS LEVEL LVE VALVE (PSI) - (PSI)-

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OJP Sn 1394 Prinnrv Mrano Pm 14500 Primary plus secondary Op Sm 3927 stress due to internal 14500 pressure 7937 Axial Pod [75 pipe , -

Body reaction ,2 1476 1 5 an stress Bending Peb P t 3, 16440 1.5 Sm

'Ibrsion Pet 21750

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5, 419 Sm Thermal secordary Ob 14500 H16) l Stress _

1 25629 3 Sm Primary plus Sn l 43500 seconv1.,ry stress l

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S(1) 3246 0.9 Cy Disc Conbined Berding 27000 f Stress on disc centerline S(9) 11988 ogg2n Torsional shear Stress 0.6 na Carbinal Shear stress S(b) 12296 imo e

14599 an Shaft Catbilial bciv. ling S (5) 22200 stress 21599 an Canbined stress S(4) 22200 (shear and bending) ~

S(16) 22318 0.9 v)

Shaft Key Shear stress on 50500 key S(17) 36308 0.9 y Disc tapper Shear stress in 31500 pins pins 1612 Conpressive allowable Bearing stress in S(21) 10000 Bushirus (chaft bearing) lxishings - -

24010 0 Operator Tension in bolts S(54) fbuntirry 4S(55)

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