TXX-8907, Nonproprietary Suppl 1 to Addl Info in Support of Evaluation of Thermal Stratification for Comanche Peak Unit 1 Pressurizer Surge Line

Nonproprietary Suppl 1 to Addl Info in Support of Evaluation of Thermal Stratification for Comanche Peak Unit 1 Pressurizer Surge Line

ML20247G985
Person / Time
Site:	Comanche Peak
Issue date:	09/30/1989
From:	Cranford E, Mutyala B, Valasek L WESTINGHOUSE ELECTRIC COMPANY, DIV OF CBS CORP.
To:
Shared Package
ML19307A355	List: ML20247G966 ML20247G977 TXX-8907, Nonproprietary Suppl 1 to Addl Info in Support of Evaluation of Thermal Stratification for Comanche Peak Unit 1 Pressurizer Surge Line
References
TXX-890706, WCAP-12247-S01, WCAP-12247-S1, NUDOCS 8909190184
Download: ML20247G985 (27)

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WESTINGHOUSE CLASS 3 WCAP-12247 Supplement 1 e 0 ~, ADDITIONAL INFORMATION IN SUPPORT OF THE EVALUATION OF THERMAL-STRATIFICATION FOR THE COMANCHE PEAK UNIT 1 PRESSURIZER SURGE LINE E. L. Cranford B. R. Mutyala L. M. Valasek R. L. Brice-Nash September 1989 Verified by: / //[f/ / Verified By: / K. C. Chang / B. J.,Coslow d u-f Seb Approved by: Sid Approvedby[: R. B. Patel, Manager

5. 5. Palusamy/ Manager Systems Structural Structural Materials Analysis Engineering l

l l } WESTINGHOUSE ELECTRIC CORPORATION Nuclear and Advanced Technology Division P.O. Box 2728 Pittsburgh, Pennsylvania 15230-2728 3027s/D01180 to i l

r 2 l l FOREWORD This supplement addresses specific questions presented by the Nuclear ~ Regulatory Commission during their review of the original WCAP-12248 of Comanche Peak Unit 1. The questions were presented to Texas Utilities. The questions and their respective responses are provided on the following pages. In addition, the supplement contains an errata section which provides corrections to typographical errors. O o. W e M =n..ia. i. 3

TABLE OF CONTENTS Section Title Page 1.0 ISSUES AND RESPONSES ON SECTION 1.0 1 . 2.0 ISSUES AND RESPONSES ON SECTION 2.0 5 3.0 ISSUES AND RESPONSES ON SECTION 3.0 11 ERRATA 17 e e A e l e g 3827s/081180 10 jj

' i-r: 9 1 LIST.0F TABLES l F..i Table Title ' Page l . S1-1~ Flow Rates and Richardson Numbers for Water Model Flow Tests- -15 l l' O e GB 4 e e l l l l l 1' l l l ll-e i k l aet?s/settes.io jjg

LIST OF FIGURES l Figure Title Page S1-1 Fatigue Calculation Locations 16 I e e h e e e l l l l as27s/osties to iy w

SECTION 1.0 )- ISSUES AND RESPONSES ON SECTION 1.0 ~ ISSUE 1-1 What is the purpose of the 1 foot section schedule 140 pipe?

RESPONSE

During installation of the pressurizer surge line in August, 1980, field fitup difficulties were encountered. In order to resolve the problem a 10 3/32" section of sch. 160 pipe was removed and replaced with a 12" section of sch. 140 pipe. The additional length (.ie. 1 29/32") relieved the fitup problem; sch. 140 pipe was used due to material availability at the site. The sch. 140 pipe satisfies Westinghouse material requirements as detailed in Westinghouse specification G-678854. ISSUE 1-2 Ne'ed to review document SSDC 1.3 which defines thermal design transients for CP-1. How was this updated? A) To reflect the monitoring data? B) From which plant? C) Were a combination of plants used or one plant (worst case) only? l

RESPONSE

SSDC 1.3 was not updated to incorporate surge line data. The monitoring data from plants A,B,C, & E (table 1-14, page 1-35) was used to create an enveloping transient set with stratifica-tion for heatup and cooldown transients. The new heatup and cooldown transients per WCAF-12248 with stratification replaced the SSDC 1.3 heatup and cooldown transients. The balance of the normal and upset transients defined in SSDC 1.3 was used in the surge line evaluation except that the transients were assumed to cause thermal stratification [ )a,c.e as27smet2se.io }

h It should'be noted that some of the transients defined in SSDC L 1.3 assume no insurge or outsurge and are therefore not 8 considered to cause thermal stratification. The combination of transients defined in Comancho Peak WCAP-12248 are considered. to conservatively envelope all 4 plants monitored. ISSUE 1 Delta T Strat = T -T Why this does not agree for press res some events of tables 1-3, 1-47 i

RESPONSE

The pressurizer and reactor coolant het leg temperatures defined in the surge line transients reflect the approximate system delta T and not the pipe delta T. Delta T I" Strat tables 1-3 and 1-4 are pipe delta T and not system delta T. ISSUE 1-4 What is'the % difference or actual values for the pipe myt's at critical locations between analytical and measured values ?

RESPONSE

See response to Issue No. 2-3 ISSUE 1-5 How were the thermal fluid conditions experienced by PSL during normal and upset transient redefined ?

RESPONSE

All normal and upset transients that were postulated to cause insurge or outsurge were [- ]"'C. The maximum system delta T was calculated regardless of simultaneity between the RCS temperature and the PZR temperature. In addition certain high cycle normal condition transients such as steady state fluctuations were [ 3a,c.e 3827s48110010 2

ISSUE 1-6. Explain tables 1-12, 1-13, 1-14, 1-15, 1-16 e A) How was this data derived and used? B)_ How do they relate to CP-17 RESPONSE: A) Table 1-12 is an example showing the approximate magnitudes of each significant cycle shown in figure 1-35; [ ya.c.e l l-l Table 1-13 shows the data used to determine the design distribution of the strength of stratification factors. This table shows the intervals used to group the strength of stratification factors and to determine their relative i distribution. [ j a. c. e' Table 1-14 shows the data used to determine the number of cycles of stratification events for one heatup for design purposes. [ 3a,c.e l Table 1-15 was developed from historical data collected from plants A & B. [ 1 i ja c.e l[ Table 1-16 shows the striping transients used in the design 4 evaluation. [ w ya.c.e nn innu se 3

~ v l B) The basis for tables 1-12 through.1-16 was actual monitoring data from four plants which did not include Comanche Peak. a Comanche Peak Unit I monitoring data from HFT was reviewed to i* confirm the conservatism of the assumptions used in the evaluation. l ISSUE 1-7 Table 1-7, What is the delta T max used ? (Page 1-12 references Delta T = 260'F, Delta T = 320*F)

RESPONSE

Delta T max of 320 deg F was used. e .g d e .e o e ' 3s27s/IS124910 4

-2 \\ c SECTION 2.0 ISSUES AND RESPONSES ON SECTION 2.0 ISSUE 2-1 Figure 2-4 What about the case of top-to-bottom Delta T = 320'F.

RESPONSE

Figure 2 -4 describes the temperature profiles in the verification analysis using the typical surge line layout of Figure 2-3. These temperature profiles were not used in the Comanche Peak Unit 1 surge line analysis. Delta T,,, of 320*F was used in the Comanche Peak Unit i surge line analysis as indicated in Tables 1-3 (page 1-22) and Section 2.1.3 (page + 2-5). ISSUE 2-2 Need to review cases of thermal stratification which have been } obtained by interpolation from the 11 cases run. l*

RESPONSE

Moment values for all individual transient cases, obtained by interpolation from 11 cases, are included in the input decks to l WECEVAL. The methodology used to'obtain these moments is. provided in the documentation. The 11 cases provide sufficient data to evaluate all the transients defined in tables 1-3 and 1-4. ISSUE 2-3 Provide maximum values and locations for a) Displacements b) Reactions c) Stresses for ASME III equations 9, 10, 11, 12, 13, 14. Need to see comparison with/without stratification 1 3827sM110010 5

I L 1 1 .l 1

RESPONSE

Maximum values and locations: 8 a. Displacements i Node 1170 of figure 2-22 corresponds to the approximate lanyard location where the comparison is made. l Measurements provided at lanyard location were as follows: A vertical displacement of 1.1 inches was observed when the pipe went froi. an unstratified condition to a stratified condition with a pipe delta T = 262*F. Analysis results at node 1170 for the same conditions produced the following: A vertical-displacement of 1.46 inches was calculated when the pipe was taken from an unstratified condition to a stratified condition with a pipe delta T of 260*F. Since monitoring data was not available at the time of the analysis a conservative temperature profile was developed. Higher vertical displacements fr:m analysis as compared to actual measured displacements are expected. b. Reactions Reactions from stratification analysis for maximum Pipe delta T = 320 F, at ends of model: Hot leg: FX = 23.9 K PZR: FX = -23.9 K FY = 3.4 K FY = -3.5 K FZ = -8.0 K FZ = 8.3 K MX = -1585 IN-K MX = -376 IN-K ~ MY = -2815 IN-K MY = 445 IN-K MZ = -5321 IN-K MZ = -1414 IN-K s Note: Reactions at the pressurizer surge nozzle for normal operating conditions produced higher loads than the maximum stratification condition, mmann in 6

c. ASME III Stresses 1) Without stratification: One case run in the stratification analysis was a normal operating condition without stratification. This case was used to benchmark the ANSYS model.

2) With stratification:

Eq. 9: Not affected by stratification; existing analyses unchanged Eq. 10: [ Ja,c.e Eq. 10 values are calculated for all combinations in elastic plastic analysis to determine penalty factor, Ke. } Eq. 11,14: Actual maximum values of these stress equations are not checked against a specific allowable stress, but are reflected in the final usage factor values. Maximum usage factor of [ 3a,c.e Eq. 12: Maximum value calculated at [ Ja,c.e and is = 52.1 ksi. Corresponding allowable stress is 35m = 57.9 ksi. Eq. 13: Values of Eq.13 from existing analyses are not affected by thermal stratification loading where no gross structural discontinuity is present. Therefore, EQ. 13 was only calculated at [ 3a,c.e A maximum value of 46.7 ksi was calculated at [ Ja.c.e Corresponding allowable stress is [ 35m = 50.1 ksi. The above results represent design basis analysis that s includes stratification. These results are also provided in table 2-11. Since the design basis analysis assumes 3827s/DB11SS.10 ]

L t stratification, a tomparison of ASME Code stresses between the results of a stratified vs. unstratified cases is not applicable. is-ISSUE 2-4 How were the FE stress indices developed ? Why code indices were not used ?

RESPONSE

ASME III code stress indices were used for all cases except [ 3a,c.e [ Ja,c.e evaluation used the results of finite element analyses for secondary stresses in lieu of code stress indices to reduce conservatism to calculate Ke factor and. Equation 12. C was defined [ 2 Ja c.e However, ASME III code K stress indices for buttwelds were conservatively applied to add conservatism. ISSUE 2-5 What are the actual / allowable values for both the hot leg.and the pressurizer nozzle?

RESPONSE

The actual loads due to all design basis leading including stratification were used to calculate cumulative usage factors at both the hot leg and the pressurizer nozr:le. Maximum usage factor of [ la c.e Maximum usage factor [ 3a c.e Equation 12 and 13 stresses [ Ja.c.e are [ shown in response to Issue No. 2-3c. Equation 12 stress of 31.9 ksi and Equation 13 stress of 37.5 ksi were calculated for [ [ )"'C Corresponding allowable stress is 3 S, = 39.6 ksi (for both Equation 12 and 13). a n. e in 8

r ISSUE 2-6 Ref. Table 2-3 and Fig. 2-22. Why T is different than bot T ? Which temperature war,used for analysis ? HL

RESPONSE

The pressurizer and RCL temperatures defined in Table 2-3 (page 2-22) reflect the approximate system delta T and not [ Ja,c.e System delta T was only used to define the boundaryconditions(thermalanchormovementsatbothendsof surgeline). [ Ja,c.e Also, see response to Issue No. 1-3. ISSUE 2-7 Table 2-5. What about thermal stresses at Delta i = 320'F?

RESPONSE

Westinghouse analyses show [ Ja,c.e; therefore, stresses for the-320*F case can be determined from the 260*F case. ISSUE 2-8 Tables 2-6, 2-7. How are these values utilized in question 3c above?

RESPONSE

Tables 2-6 and 2-7 show stresses calculated from finite element models [ la.c.e Values were obtained :or each transient load case by superposition of stresses due to the various loadings. Actual stress for a given loading was obtained using ratios based on specific load case parameters. { 3a,c.e

7 Lead case pressure and delta T are obtained from the transient

a definition.

[ P.. Ja,c.e This is more fully described in the calculation packages. l l ISSUE 2-9 Figure 2-55. How were these results modified to be used for the CP-1 PSL7

RESPONSE

The flow model test results are used to obtain frequency and duration parameters which are used in the striping evaluation. The frequency and duration parameters are considered to be functions of the flow rate and buoyancy forces between the hot and cold water interface, and not pipe diameter and wall thickness. [ ~'. Ja,c.e The total calculated usage factor for striping has been increased by 50 percent to account for any uncertainty in the selection of frequency or other variables. 4 mwneme in 10

L 1 SECTION 3.0 ISSUES AND RESPONSES ON SECTION 3.0 s ISSUE 3-1 Which are the five cases used? How were these determined to be the worst case?

RESPONSE

In the plant-specific analysis, [ Ja,c.e The five worst cases selected in the fatigue analysis are the in-line component in each profile region with I the highest C and K stress indices defined by the ASME Code. At SD bends, K indices for buttwelds were conservatively applied to add conservatism. ISSUE 3-2 Need to discuss the superposition technique on the stress component basis. How were the " appropriate factors to account for specific transients and load cases" determined?

RESPONSE

For a given load condition, the total stress in the pipe is determined by superposition of stresses due to pressure, moment and local stratification effects. The stresses in the finite element model due to each of these types of loading were first determined for nominal values of load and stored on computer tapes. [ "a umann in 11

g o;. ja,c.e Scale factors were then developed for each load condition based on actual pressure, moment and stratification loading for each condition and stress indices for the component being evaluated. [ } Ja.c.e C and C2 are determined y from ASME Code Subsection NB-3681 for the component being I.. evaluated. l i The total stress at each node point in the finite element model is then determined by superposition of the individual l ~ contributions as follows. ) L i

• 1, ls I

l i m m o n. i. 12

b*% a. ja,c.e The finite element model stresses on tape are the c.x stress ~ components at each node point in the model. After determining the total stress components for each load condition defined in Tables 1-3 and 1-4, program WECEVAL proceeds with the fatigue evaluation according to NB-3222.4. In the evaluation, peak effects are conservatively considered by applying the maximum peak stress index from NB-3681 (K, 3 K ' E ) f r the component being' evaluated to the total 2 3 stress. ~ 'I ISSUE 3-3 For which cases ( a) ASME III cede stress indices were used? b) F.E. stress concentrations effects were utilized?

RESPONSE

a) ASME B&PV Code Section III stress indices were used for all cases except [ Ja,c.e b) [ Ja,c.e evaluation used the results of finite element analyses for secondary stresses in lieu of Code stress indices. ISSUE 3-4 Which 17 sections were evaluated for the usage factors? How was it determined that these are the worst cases? What are the [ values?

RESPONSE

The mesh of the finite element model is such that 17 cross s sectional cuts are defined by the element boundaries and node points in the circumferential direction (see attached Figure serwnenseae 13

S1-1). Thus, the 17 sections virtually comprise the entire f model. The values of stress at each section for e6ch loading are contained on computer tapes used in the evaluation. Usage factors were calculated at selected node points in the finite element model on the pipe wall surface, corresponding to the analysis sections. These node points were selected based on review of the local stress profiles and previous analysis results where maximum usage factors were calculated. [ Ja,c.e The maximum usage factor was then reported for the global location (figure S1-1 provides the results for global location 5). ISSUE 3-5 At which location and for which load cases ASME III NB-3600 equation 10 was exceeded? What was the value?

RESPONSE

ASME Equation 10 is calculated by WECEVAL for every combination at each cross section evaluated at each global location to determine the elastic plastic penalty factors, Ke. The values of Ke are stored on tape to be used in the subsequent usage factor calculation. l The various locations for which Eq. 10 was exceeded can be obtained by detailed review of the computer runs. In the whole of the analysis, [ ja.c.e Due to the nature of the thermal stratification loading. [ Ja,c.e is the more critical for qualification. ~ 3 mmmme in 14

ji l TABLE S1-1 FLOW RATES AND RICHARDSON NUMBERS FOR WATER MODEL FLOW TESTS s Pipe Section Cold Water Flow Rate (GPM) Ri a,c.e 4.0 inch I.D. 6.5 inch I.D. 4 4 9 A 9 k un.'"""" 15

a,c.e i.:. n - a l l 1 1. \\.. es c. 1. l l l l-s. ~ 1s Figure S1-1. Fatigue Calculation Locations m m a n n io 16 1

'T la ERRATA / N The following pages contained typographical errors. The corrections are shown with vertical lines on the right hand border. NOTE:- The corrections provided here do not change any of the conclusions /results of the original WCAP-12248, 1 l' l 9 l l l e N. i!* 1. "o mmann io 17

l - TABLE 1-13 j

SUMMARY

OF PLANT MONITORING HEATUP/COOLDOWN TRANSIENTS L.- WITH STRENGTH OF STRATIFICATION (RSS) g ja.c.e 7 ja,c.e g 3a,c.e observed Observed Observed Cycles RSS(1) Cycles RSS (1) Cycles RSS (1) a,c.e OBSERVED TRANSIENTS GRD;' PED BY STRENGTH OF STRATIFICATION (RSS). INTERVALS No. Observed % of RSS Cycles Total a,c.e [ Note: The No. of groups is reduced by combining the intervals.70 < x <.8 and.60 < x <.70 % of total = 3.2% for the interval-l .60 < x <.80-un.aii.e in 1-33

i m TABLE 1-13 (cont.) g;

SUMMARY

.0F PLANT MONITORING HEATU?/COOLDOWN TRANSIENTS b;; WITH STRENGTH OF STRATIFICATION (RSS) s. RSS J % of Transients a,c.e l-l RELATIVE NUMBER OF CYCLES OF STRENGTH OF STRATIFICATION (RNSSj) AFTER GROUPING 'uf. RSSj 4 RNSSj Strength of % Transients (2) j Stratification (1) a,c.e L. Nomenclature: (1) Strength of Stratification (RSS), (2) Relative Number of Cycles of Strength of Stratification (RNSS) A N 1 ', le mv mum;io 1 34

y-1 !s TABLE 1-14 A

SUMMARY

OF MONITORED TRANSIENT CYCLES (ONE HEATUP) .- 4 Plant No. of Cycles a,c.e Av2. Monitored Cycles: '15.75 = x; Selected No. of Design Cycles: 36.5 (added 30% to observed maximum number of '{ cycles, plant A) DESIGN DISTRIBUTION APPLIED TO MAX NUMBER OF TRANSIENTS EXCEPTED MULTIPLIED BY 200 HEATUP OR C00LDOWN CYCLES No. of Transients RSS a,c.e e an.non.so 1-35

TABLE 5-8 p

SUMMARY

OF LOADS AND STRESSES AT THE CRITICAL LOCATION Force Stress Moment Stress Total Node Case F (1bs) op(psi) M (in-lbs) oN(psi) Stress (psi) 1010" A 222878 4458 1069639 7293 11751 1010 [ Ja.c.e 1010 D 240526 4811 3436696 23433 28244 1010 [ Ja.c.e 1010 [ la.c.e l " Dimensions: 0.D. = 14 in,, minimum wall thickness = 1.249 in. bStratification AT is [ Ja,c.e ,M i 6 l an.=nn.io 5-15 -_ _ _ -_ - _ _ _ _ _ _ _ _}}