ML20066D398

Draft Pressure-Temp Curves,Per Reg Guide 1.99,Rev 2

ML20066D398
Person / Time
Site:	Oyster Creek
Issue date:	11/30/1990
From:	Caine T, Ranganath S, Swift T GENERAL ELECTRIC CO.
To:
Shared Package
ML20066D374	List: ML20066D373 ML20066D379 ML20066D387 ML20066D398
References
RTR-REGGD-01.099, RTR-REGGD-1.099 SASR-90-89-DRFT, NUDOCS 9101150035
Download: ML20066D398 (52)

Text

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SASR 90 89 gv- DRF 137 0010 November 1990 0

PRESSURE-TEMPERATURE CURVES PER REGULATORY CUIDE 1.99, REVISION 2 10=

FOR Tile OYSTER CREEK NUCLEAR GENERATING STATION t

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i Prepared by: ,

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T. A. Caine, Senior Engineer l0 q Materials Monitoring &

Structural Analysis' Services Q

Verified by: //. h TiJ. Swift,Ekgineer. I

h. ,

Materials Monitoring &

Structural Analysis Services

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Reviewed by

- h S.RanganathkManager Materials Monitoring &

'O- Structural Analysis Services 91011500ss vio111 GENuclearEnergy

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'fDR ADOCK 05000219 PDR

IMPORTANT NOTICE RECARDING p CONTENTS OF THIS REPORT PLEASE READ CAREFULLY This report was prepared by the General Electric Company. The

g. information contained in this report is believed by General Electric to be an accurate and true representation of the facts known, obtained or provided to General Electric at the time this report was prepared, g The only undertakings of the General Electric Company respecting information in this document are contained in the contract between the customer and the General Electric Company, as identified in the purchase order for this report, and nothing contained in this Cacument shall be construed as g changine,said contract, The use of this information except as defined by said contract, or for any purpose other than that for which it is intended, is not authorized; and with respect to any such unauthorized use, neither General Electric Company nor any of the contributors to this document makes any

, representation or warranty (express or implied) aa to the completeness, accuracy or usefulness of the information contained in this document or that such use of such information may not infringe privately owned rights; nor do they assume any responsibility for liability or damage of any kind which may

, result from such use of such information.

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r TABLE OF CONTENTS 3 JOj Este l

'1.0 d INTRODUCTION 11 f(y: 2.0 -Ll INITIAL REFERENCE TEMPERATURES 2-1

-r 3.0 ~ . ADJUSTED REFERENCE TEMPERATURES FOR BELTLINE 31 3.11 Rev 2 Methods-31 ,

3.2 Limiting Beltline Material 31 z):

3.2.1 Chemistry 3 2- l 3.2.2 Fluence 32 3.3 = ART vs EFPY 33

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4.0 RPRESSURE TEMPERATURE: CURVES 41 4.1' Background- 4-1_

14.21Non Beltline Regions 4 1-4 3-

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4.2;1 ( Non Beltline. Monitoring During

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-Pressure Tests 4.3 ' Core ~ Beltline Region 4-4  ;

4.4 Closure Flange. Region ~ 4-5  ;

j); /4.5 . Core CriticalL operation Re'quirements of:

J 46:

100FR50(Appendix'G -?

.5.0.: REFERENCES. 5-1 3C)1

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= APPENDICES e

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A . CHARPYLCURVES.0F SELECTED VESSEL PLATES B BELTLINE' P T CURVE CALCULATION-METHOD B-1 -

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g. -C IMPACT ON P T CURVES OF HEATUP/COOLDOWN RATE C1 o

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1.0 INTRODUCTION

0-The pressure temperature (P T) curves in the Technical Specifications are established to the requirements of 10CFR50, Appendix 0 (1) to assure that brittle fracture of the reactor vessel is prevented. Part of the analysis

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O-embrittlement effects in the core region, or beltline. The method used to account for irradiation embrittlement is described in Regulatory Guide 1.99, Revision 2 (2), or Rev 2.

O In addition to beltline considerations, there are non beltline discontinuity limits at nozzles, penetrations and flanges which affect the P T curves. The non beltline limits are based on generic m1yses which are adjusted to the maximum reference temperature (RTNDT) fo; the applicable Oyste* Creek vessel components. The non beltline limits are also governed by requirements in (1), based on the closure flange region RTNDT.

This report presents P T curves incorporating irradiation effects for the beltline per Rev 2 and appropriate non beltline limits. The curves have been developed to present steam dome pressure versus minimum vessel metal temperature. In addition, a refinement has been made which may minimize heating requirements prior to pressure testing, specifically:

- A. curve has been-included to allow monitoring of the non beltline regions of the vessel, such as the bottom head, separate from the beltline, The report contains a description of the methods used to calculate P T linits and has example calculations for the v'ssel beltline for pressure testing and hettup/cooldovn conditions.

Temperature monitoring requirements and moth'ds are available in CE Services Information Letter (StL) 430. The specific issue os maintaining a heatup or cooldown rate of 100'F/hr, as it relates to the P-T curves, is g

discussed in this-report.

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j 2.0 INITIAL REFERENCE TEMPERATURES Q.

In order to perform a complete analysis of the vessel P T requirements,- i initial- RTNDT values are needed for all low alloy steel vessel components.1 The requirements for establishing the vessel component toughness per the ASME

! Code prior to 1972 are summarized as follows:

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a. Test specimens shall be longitudinally oriented Charpy V Notch-  !

specimens,

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b, At the qualification test temperature (specified in vessel purchase specification), no -impact _ test' result shall be less than 25 ft lb',

-and the average.of'three test results shall be at least 30 ft lb..

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c. Pressure tests shall be' conducted at a temperature'at least-60'F -(

above the. qualification test temperatuce for the vessel materials.

The current requirements establish a RTNDT value, and are significantly-differents For plants constructed to the ASME Code after Summer 1972 the requirements are as follows:: .;

a. Charpy V Notch specimens shall be 1 oriented normal ' to the ' rolling directiony(transverse),

s b.' 'RTNDT is defined as the~ higher of the. dropweight:NDT or 60*F'below g_ the temperature at which Charpy;..V Notch 50.ft-lb energy and 35 mils lateral expansion are met,

c. Bolt up-in preparation for_a pressure test or normal operation. l j

.shall be' performed at or above~ theLRTNDT or lowest service temperature'(LST). whichever is greater.

".i-100FR,50 Appendix -G states that for vessels-constructed to a version of. ,

the ASME Codt prior to the Summer 1972 Addendum, fracture toughness. data and g ,

data analyses must be supplemented in an approved manner. CE has developed

, methods for analytically. converting fracture toughness data for vessels

- constructed before 1972 to comply with current requirements. GE developed 21

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these nethots from data in k'RC Bulletin 217 (3) and from data collected to respond to NRC questions on TSAR submittals in the late 1970s. The CE nethoda  :

O have not been generically approved by the NRC, but they have been accepted on a case by case basis in submittals by about 20 utilities. The data used in developing the CE nethods cover A533 plate materini and submerged are and shielded metal are welds. Since the Oyster Creek vessel plates are 302B O natecial, some su o semental evaluation of RTuor has been done in this report on some of the vessel plates. These nethods and example RTNDT calculations for vessel plate, weld, veld HA2, forging, and buting naterial are summarized in the remainder of this section. Calculated RTHDT values for selected RpV

,O locations are given in Tabie 2 1.

For vessel plate material, the first step in calculating RTNDT 18 to establish the 50 f t lb transverse test temperature from longitudinal test O ,p,ct,,n e,t,, .ihere are typically three energy values at a given test temperature. The lowest energy Charpy value is adjusted by adding 2'r per ft lb energy to 50 ft lb. For example, for plate 0 309 2 in the closure head, the test teroperature and lowest Charpy energy from Table 2 1 is 28.5 ft lb at O 41o.F. The equivalent 50 ft ib longitudinal test temperature is:

T30L - 10'F + !(50 28.5) f t lb

• 2'F/f t lb) - 53*r

1. The transition from longitudinal data to transverse data ic nade by adding 30'F to the test temperature. In this case, the 50 f t lb transverse Charpy test temperature is T50T - 83'F. The RTNDT is the greater of NDT or (T50T

• 60'F). The value based on Charpy data, (T50T 60'F), is 23'F. For O Oyster Creek materials, dropweight testing to estabitsh NDT was not performed, but NRC Branch Technical position MTEB 5 2 [4] recommends that NDT be estimated as the 30 ft lb Charpy test temperature, which in this case is 10'F.

Thus, the RTNDT for plate 0 309 2 is 23'F. Note that the conservative nature O of estimating T3 or will aivays result in the estimated (T 3or - 60'F) value being higher than the estimated NDT.

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Some of the 302B plate materials used in the Oyster Creek vessel exhibit  !

a rather 1 w upper shelf energy (usE). Fortunately, there are full Charpy O In examining the Charpy curves, it was found that curves for these materials.

the 2'r per it lb correction was not conservative for the materials with lower USE values. In these cases, the Charpy data were fit with a hyperbolic tangent relati nship to determine the best nstimate T $ot,. The standard O deviation of the data relative to the curve fit (by temperature) was calculated to serve as cI for the beltline materials. For non beltline materials, the value of T50L used to determine RTHDT was the besc. estimate Value plus twice the standard deviation. Plots of the Charpy curves for all O of the beltline plates and for the most limiting non beltline plates with low USE are pNvided in Appendix A. The RTNDT values in Table 21 for these plates are based on the Appendix A curves.

O For vessel veld material, the Charpy V Notch results are usually more limiting than dropweight results in establishing RTHDT. The 50 f t lb test temperature is established as for the plate material, but the 30'F adjustment

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O metal. For example, weld heat 86054B with flux lot 4D4F has a lowest Charpy energy of 29 f t lb at 10'F. The 2'F per f t lb adjustment gives a T50T value of 52'F. The GE procedure requires that, when no NDT is available, the <

resulting RTNDT be 50'F or higher. In this example, (T507 60't) is 8'F, O

so the RTNDT is 8'F. Since the method of estimating RTHDT operates on the lowest Charpy energy value, and provides a conservative adjustment to the 50 f t lb level, the value of og is taken to be O'F.

O-For the vessel weld llAZ material, the RTNDT is assurned to be the same as for the base material since ASME Code veld procedure qualification test requirements and post weld heat treat data indicate this assumption is valid.

O For vessel forging material, such as nozzles and closure flanges the method for establishing RTNDT is the same as for vessel plate material. For the CRD return nozzle G 319, the lowest Charpy data at 40'T is 25 f t lb. In this cas . (T50T 60'F) is (40 + (50 25)*2 + 30 60), or 60*F.

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For bolting material, the current ASME Code requirements define the LST l as the tmperature at which transverse Charpy, V. Notch energy of 45 f t.lb and

) 25' ails lateral expansion (MLE) are t.chieved. If the required Charpy results are not met, or are not reported, but the Charpy V. Notch energy reported is above 30 ft.lb, the requirements of the ASME Code at construction are applied, namely that the 30 ft.lb test temperature plus 60*F is the LST for the bolting  !

) materials. Charpy data for the studs did not meet the 45 ft-lb, 25 MLE requirement, but 30 f t lb energies were met at 10'F. Therefore, the bolting material LST is 70'F.

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Table 2 1 INITIAL RTNDT VALUES OT 15ELTLINE AND OT}lER SELECTED RPV MATERIALS

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Test Charpy' T 60 o RT

Ident. Heat Temp, Energy 50T I NDT Lgention Number - Nunber LI), (ft lb) ('F) ,(m E q_

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Lower Shell Plates C 307 1 T1937 2 see App. A 30 12.6 (a)

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G 308 1 T1937 1 see App. A 21 14.2 (a) 0 307 5 P2076 2 see App. A 3 13.9 (a)

L wer Internediate C87 P2161 1 see App. A 17 10.7 (a)

O Shell Plates C88 P2136 2 see App. A B 12.8 (a) 0.B 6 P2150 1 see App. A 31 12.7 (a)

Lower Long, 2 564 8605415 10 64,65,66 50 0.0 50 Wids A ,11, C Lot 4E$r

'D Lower Int. Long. 2 564 86054b 10 20,31.5,32 8 0,0 8 Velds 0,0,r Lot 4D4r Lower to Lower Int. 3 564 1248 10 $3.5,57.65 50 0.0 50 cirth veld tot 4M2r lO 1 Non l\citling:

vpper Shell riate c.307 n1 r2112 2 6ee App. A 25 5.3 36(b)

O Vessel Flange 0 306 X.43162 10 92,143,153 20 0.0 20 1

2 lload Finnge 0 305 X.43162 10 212,261,261 20 0.0 20 T p ilead T rus -c 309 2 r2074 1 10 28.5,35.39.5 23 0.0 23

O Bottom llcad Torus 0 301 4 A7153 2 see App A 45 10.3 66(b)

CRD Return Nozzle 0 319 BT 1676 40 25,34,38 60 0.0 60 Recirc Inlet Forg. C.312 1 D 6936 2 10 28.5,30.5,31 23 0.0 23 iO 2

(a) 60) and v are used in Section 3 according to the The values of (T50T "ethods in Rev ')

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(b) The RT NDT values r these non4citline matnials are the (T 50T * ' ' P ""

20 3

2*b 10

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3,0 ADJUSTED REFERENCE TEMPERATURES FOR BELTLINE )

10 The adjusted reference temperature (ART) of the limiting beltline material is used to correct the beltline P T curves to account for irradiation J effects. Rev 2 provides the methods for determining the ART. These nethods, f

Q and the limiting material properties used, are discussed in this section.

3.1 REV 2 METil0DS O The value of ART is corrputed by adding the S1111T term for a given value of effective full power years (EFPY) to the initial RTNDT. For Rev 2, the S11117 equation consists of two terms:

O SilI}T - ARTNOT + Margin 0.10 log f) where ARTNDT - [CF]*f(0.28 Hargin = 2(o18 4 e68 )0.5 eO f - fluence for the given EFPY / 10 19 Chemistry factors (CF) are tabulated for welds and plates in 'lanles 1 and 2,

.O respectively, of Rev 2. The margin term oA has set values in Rev 2 of 17'F for plate and 28'F for veld, flowever, og need not be greater than 0.5*ARTgpT.

Uncertainty on initial RTNDT. 01, is discussed in Section 2.0.

O 3.2 LIMITING BELTLINE MATERIAL An evaluation of all beltline plates and submerged are welds was made, and is summarized in Tables 31 and 3 2. The inputs used in determining the

O timiting beltline material are discussed in the remainder of this section.

~O Q 31

p b 3.2.1 Chemistry The vessel material certification records provided much of the detail of the beltline material chemistries, llowever, critical information on copper and, in some cases nickel, were not provided with the material certificates.

, CPUN established values for the missing data in Technical Dats Report (TDR) 725 [5). The data from the material records and from TDR 725 are presented in Table 3 3. The copper and nickel values shovr there were used in the Rev 2 calculations.

3.2.2 Fluence The Oys.ter Creek surveillance test report [6] presents a calculated y

value of 32 ETPY fluence at the inside vessel surface. GPUN made an adjustment to the value in [6] to reflect some new information on power history, resulting in a ';2 EFPY fluence of 3.74x10 18 n/cm2 reported in TDR 725. CE has just completed an evaluation of lead factor (fluence ratio

, between the surveillance capsule and the vessel peak) and has computed values very close to those in (6). Therefore, the fluence value in TDR 725 is used in the Rev 2 calculations, g

Rev 2 provides a method of calculating the vessel 1/4 T fluence based on the fluence at the vessel inside surface, fsurf. llowever, Rev 2 niso allows for the use of displacement per atom (dpa) analysis to determine the attenuatior, to the 1/4 T location. A dpa analysis was performod in (6),

p resulting in an attenuation relationship as follows:

f1/4 7 - 0.63

• fsurf g

The resulting 1/4 T fluence is:

18 f1/4 T - 2.36x10 n/cm2 p This 1/4 T fluence is about 3% less than the value calculated with the attenuation relationship in Rev 2.

, 32

l 3.3 ART VS EPPY Combining the inputs of initial RTHDT, chemistry and fluence, Rev 2 is used to compute ART as a function of EFPY. Table 31 shows ART values for 32 ETPY of operation. Table 3 2 shows ART for 17 ETPY of operation. In both cases, plate C 8 6 has the highest ART, due to the f act that it also has the highest initial RTNDT. The limiting submerged arc veld has a higher SilIFT value, but a lower initial RTNDT such that the ART is less than that of the plate. Therefore, plate G 8 6 is the limiting material throughout the operating period of 32 EFPY. ART is plotted versus ETPY in Figure 31. The ART values at 17 and 32 EPPY are used in the P T curve development in Section 4.

3-3 l

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v v Table 3-1 BELTLINE EVALUATION FOR OYSTER CREEK AT 32 EFPY OF OPERATION Shell Thickness'= 7.125 inches Peak I.D.-' fluence = 3.74E+18 Peak 1/4 T fluence =2.36E+18 Initial 32 ETPY 32 ETPY 32 EFPY

%Cu %Ni CF 'RTndt Sigma-I Delta RTndt Margin Shift ART COMPONENT .I.D. HEAT OR HEAT / LOT PLATES:

G-307-1 T-1937 0.17 0.11 79.5 30 12.6 48.4 42.3 90.8 120.8 Lower Shell Lower Shell G-308-1 T-1937-1 0.17 0.11 79.5 21 14.2 48.4 44.3 92.7 113.7 43.9 149.9 152.9 Y

n Lower Shell G-307-5 P-2976-2 0.27 0.53 173.9 3 13.9 106.0 Low-Int Shell -G-8-7 P-2161-1 0.21 0.48 139.4 17 10.7 84.9 40.2 125.1 142.1 Low-Int Shell 'G-8-8 :P-2136-2 0.18 0.46 120.7 8 12.8 73.5 42.6 116.1 124.1 Low-Int Shell .G-8-6 P-2150-1 0.2 0.51' 138.2 31 12.7 84.2 42.4 126.6 157.6 WELDS:

Lower Long. 2-564 86054B, ARCOS' O.35 0.2 168 -50 0 102.4 56.0 158.4 108.4 A,B,C FLUX LOT 4ESF 2

Low-Int Long. 2-564 860548, ARCOS 0.35 0.2 168 -8 0 102.4 56.0 158.4 150.4 D,E,F FLUX LOT 4D4F Lower to. 3-564 1248, ARCO 3' 0.22 0.11 105.3 -50 0 64.2 56.0 120.2 70.2 Low-Int Girth FLUX LOT 4M2F

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O Table 3-2 BELTLINE EVALUATION FOR OYSTER CREEK AT 17 EFPY OF OPERATION Shell Thickness = 7.125 inches Peak I.D. fluence = 1.99E+18 Peak 1/4 T fluence =1.2SE+18 i Initial 17 EFPY 17 EFPY 17 EFTY I ART COMPONENT I.D. HEAT OR HEAT / LOT %Cu 1Ni CF RTndt Sigma-I Delta RTndt Margin Shift PLANS:

Lower Shell G-307-1 T-1937-2 0.17 0.11 79.5 30 12.6 36.8 42.3 79.2 109.2 Lower Shell G-308-1 T-1937-1 0.17 0.11 79.5 21 14.2 36.8 44.3 81.1 102.1 43.9 124.5 127.5 Y Lower Shell w

G-307-5 P-2076-2 0.27 0.53 173.9 3 13.9 80.6 Low-Int Shell G-8-7 P-2161-1 0.21 0.48 139.4 17 10.7 64.6 40.2 104.8 121.8 )

Low-Int Shell G-8-8 P-2136-2 0.18 0.46 120.7 8 12.8 55.9 42.6 98.5 106.5 Low-Int Shell G-8-6 P-2150-1 0.2 0.51 138.2 31 12.7 64.0 42.4 106.5 137.5 i

WELDS:

Lowr Long. 2-564- 86054B, ARCOS 0.35 0.2 168 -50 0 77.8 56.0 133.8 83.8 i A,B,C FLUX LOT 4ESF i

Low-Int Long. 2-564 860543, ARCOS 0.35 0.2 168 -8 0 77.8 56.0 133.8 125.8 j D,E,F FLUX LOY 4D47 ,

Lowr to 3-564 1248, ARCOS 0.22 0.11 105.3 -50 0 48.8 48.8 97.6 47.6 j Low-Int Girth FLUX LOT 4M2F I

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Table 3-3 CHEMICAL COMF051 TION OF RFV BELTLINE MATERIALS Co:noosition by Veicht Percent S Si_ Ni Mo .Cu Heat / Lot No. C Mn F_

Identification Iower Shell Plates: 0.011 0.022 0.24 0.11

• 0.51 0.17

• G-307-1 T1937-2 0.2 1.4 0.17 #*

1.4 0.011 0.022 0.24 0.11

• 0.51 G-308-1 T1937-1 0.2 0.52 0.27 0.2 1.28 0.019 0.030 0.21 0.53 G- 307-5 P2076-2 Iower-Intermediate Shell Plates. 1.35 0.019 0.021 0.24 0.48 0.46 0.21

• G-8-7 P2161-1 0.19 0.4~,' O.18

• 0.19 1.36 0.006 0.024 0.26 0.46 G-8-8 P2136-2 0.51 0.46 0.20

• P2150-1 0.2 1.25 0.013 0.026 0.23 G-8-6 Lower Shell longitudinal Velds: 0.02 0.34 0.2

• 0.51 0.35

• RACOf3, 86054B 0.12 1.54 0.015 2-564 A,B,C ARCOS B-5 Iot 4E5F Iower-Intermediate longitudinal Veld: 0.2

• O.50 0.35

• 0.12 1.67 0.013 0.02 0.41 2-566 RAC0f3. 86054B D,E,F ARCOS B-5 Lot 4D4F Lower to Iower-Intermediate Girth Veld: 1.26 0.015 0.02 0.22 0.11

• 0.57 0.22

• 3-564 RAcof3, 1248 0.097 ARCOS B-5 Iot 4M2F Values reported in TDR 725.

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4.0 PRESSURE TEMPERATURE CURVES f

) l 4.1 BACKCROUND Operating limits for pressure and temperature are required for three

) categories of operation: (a) hydrostatic pressure tests and leak tests, referred to as Curve A; (b) non nuclear heatup/cooldown and low level physics tests, referred to as Curve B; and (c) core critical operation, referred to as Curve C. There are three vessel regions that affect the operating limits:

) the closure flange region, the core beltline region, and the remainder of the j vessel, or non beltline regions. The closure flange region limits are l controlling at lower pressures primarily because of 10CFR50 Appendix C [1]

requirements. The non beltline and beltline region operating limits are

) evaluated according to procedures in 10CFR50 Appendix C, Appendix C of the ASME Code [7] and Welding Research Council (VRC) Bulletin 175 [8), with the beltlino region minimum temperature limits adjusted to account for vessel irradiation.

)

Figure 41 has curves applicable, per Rev 2, for 17 EFPY of operation.

Figure 4 2 has curves applicable for 32 EFPY, The requirements for each vessel region influencing the P.T curves are discussed below.

) Tables 4 1 and 4 2 have tabulations of the P.T values for Figures 4 1 and 4 2, respectively.

4.2 NON. BELTLINE REGIONS

)

Non-beltline regions are those locations that receive too little fluence to cause any RTNDT increase. Non beltline components include the nozzles, the closure flanges, some shell plates, top and bottom head plates and the control

) rod drive (CRD) penetrations, Detailed stress analyses, specifically for the purpose of fracture toughness analysis, of the non beltline components were

_performed for the BWR/6. The analyses took into account all mechanical loadings and thermal transients anticipated, Transients considered included

) 100'F/hr startup and shutdown, SCRAM, loss of feedwater heaters or flow, loss of recirculation pump flow, and all transients involving emergency core 41

)

O

) O cooling injections. Primary membrane and bending stresses and secondary membrane and bending stresses due to the most severe of these transients were

)

used according to [7] to develop plots of allowable pressure (P) versus temperature relative to the reference temperature (T RTNDT). Plots were developed for the two most limiting BVR/6 regions; the feedwater nozzle and the CRD penetration regions. All other non beltline regions are categorized

)

under one of these two regions.

The BVR/6 results have been applied to earlier BVR non beltline vessel components, based on the facts that earlier vessel component geometries are

)

not significantly different from BWR/6 configurations and mechanical and thermal loadings are comparable.

The BVR/6 non beltline region results were applied to Oyster Creek by

) adding the highest Oyster Creek RTNDT values for the non beltline discontinuities to the appropriate P versus (T RTNDT) curves for the BVR/6 CRD penetration or feedwater nozzle. Table 2 1 shows the most limiting non beltline RTNDT values for the non beltline components. The CRD return

) The nozzle RTHDT of 60'F is used with the BWR/6 feedwater nozzle curve.

bottom head RTNDT of 66'F is used with the CRD penetration curve.

There are two nozzles in the Oyster Creek vessel which are not found in

) later BVR vessels. These are the recirculation inlet nozzle and the isolation condenser nozzle. These nozzles were reviewed to assure that the limits developed for BWR/6 would apply.

) The recirculation inlet nozzle is a 1,41 inch thick ring forging welded to the outside of the vessel at the inlet penetration. Since the forging is less than 2.5 inches thick, it is exempt from fracture toughness analysis per ASME Appendix C, paragraph G 2223(c), as long as the RTNDT is at least 60'F

) below the lowest service temperature, Table 2 1 shows the RTNDT for the forging, 23*F. This is more than 60'F below the lowest service temperature for this nozzle, based on a boltup temperature of 85'F, so adequate fracture toughness is. assured.

)

42

4

) .

The isolation condenser nozzle is approxinately the sarsc geonetry as the

)

feedwater nozzle, The Oyster Creek stress report [9] states that the therit.a1 stresses for the feedwater nozzle are more severe than those for the isolation condenser nozzle. Therefore, the Bk'R/6 feedwater nozzle limits, adjusted to the highest RTNDT for Oyster Creek nozzles, vill provide conservative p T

) limits for the isolation condenser nozzle.

4.2.1 Non Beltline Monitorine Durint Pressure Tests

) While the beltline curves are limiting for pressure test conditions, the non beltline limits can still be applied to the other regions of the vessel.

It is likely that, during leak and hydrostatic pressure testing, the bottorn head or top head temperature may be significantly cooler than the beltline.

This condition can occur in the bottoin head when the recirculation punps are

)

operating at low speed, or are off, and injection through the control rod drives is used to pressurize the vessel. i t. is also possible that heat losses

~

from the top head could make it difficult to rtaintain the same teitperatures as g those in the beltline.

Monitoring the bottom head or top head separately from the beltline region may reduce the required pressure test temperature by 10'T to 20'F.

p Some hypothetical teroperatures demonstrating the potential benefit of separate bottom head monitoring are shown in Figure 4 3. The Technical Specifications currently require that s.11 vessel temperatures be above the listiting conditions on the P T curve. That would mean that, for a leak test, the g bottom head would have to be heated above 203'F at 17 EFpY as shown in case (a) of Figure 4 3, The bottom head ternperature reading would likely be the limiting reading on the vessel during the test, If, by using the bottorn head curve, the required teroperature for the bottom head were only 187'F, the p limiting reading would probably be near the beltline, as shown in case (b),

and the actual vessel temperatures could be lowered cortpared to case (a).

One condition on monitoring the bottom head or top head separately is y that it must be demonstrated that the vessel beltline temperature can be accurately monitored during pressure testing. An experiment has been conducted at a Bk'R 4 which showed that thermocouples on the vessel near the p 43

O .

feedwater nozzles, or temperature measurements of water in the recirculation loops provide good estimates of the beltline temperature during pressure O testing. OpVN may need to confirm this before implementing separate monitoring of the bottom head or top head. First, however, it should be determined whether there are significant temperature differences between the beltline region and the bottom head or top head regions.

4.3 CORE BELTLINE REGION The pressure temperature (p T) limits for the beltline region are O determined according to the methods in ASME Code Appendix 0 [7). As the beltline fluence increases during operation, these curves shif t by an amount discussed in Section 3. Typically, the beltline curves shift to becomo more limiting than the non beltline curves at some point during operating life.

O For the Oyster Creek vessel, the non beltline curves were limiting through about 7 EFpY, at which point the beltline curves became more limiting at typical operating pressures.

O The stiess intensity factors (K I ), calculated for the beltline region according to ASME Appendix C procedures, were based on a combination of pressure and thermal stresses for a 1/4 T flaw in a flat plate. The pressure stresses were calculated using thin walled cylinder equations. Thermal O stresses were calculated assuming the through wall temperature distribution of a flat plate subjected to a 100'F/hr thermal gradient. The ART values shown on Figure 31 were used to adjust the (T RTNDT) values from Figure G 2210 1 of (7). More details on the methods used in computing beltline curves are O contained in Appendix B.

The beltline p T curves are calculated assuming an instantaneous heatup/cooldown rate of 100'F/hr. It is permitted to exceed this rate in the O Technical Specification, as long as a 100'F change in any one hour period is not exceeded (also note that exceeding the 100'F/hr rate should not be normal practice). The impact on the P.T curves of heatup/cooldown rates in excess of 100'F/hr is discussed in Appendix C.

44 O

D 4.4 CLOSURE FLANCE RECION D 10CFR50 Appendix C sets several minimum requirements for pressure and temperature, in addition to those outlined in the ASME Code, based on the closure flange region RTNDT. In some cases, the results of analysis for other regions exceed these requirements and they do not affect the shape of the F T D curves. However, some closure flange requirements do istpact the curves. In addition, General Electric has cotapared the current requirements and the original requirements in determining the minitoum boltup teteperature.

O The current boltup teroperature of 100'r is based on the assumption that materials were qualified to meet 30 ft lb Charpy energy at 40'F, based on the vessel purchase specification. The original Code requirement was that boltup be done at qualification temperature (T30t) plus 60'F, Current Code requirements state, in Faragraph C 2222(c) of [7), that for application of full bolt preload and reactor pressure up to 20% of hydrostatic test pressure, the RFV metal tettperature taust be at RTNDT or greater. The approach used for Oyster Creek is to determine the highest value of (T30L + 60) and the hi 6hest O value of RTNDT and base the boltup teleperature on the tnore conservative value.

Table 2 1 shows the RTNDT values for the closure flanges, the limiting closure head plate connected to the closure head flange and the litaiting upper

• shell plate connected to the vessel flange, Connecting veld inaterials are not shown because they are less limiting than the plates. Table 2 1 shows the highest RTNDT for the closure region to be 36'F for upper shell plate C 307 RI. Figure 4 4 shows the Charpy curve for C 307 R1, The value of T30L

• is shown as 14'F, with 201 - 10.6'F, so that T30L can be conservatively estimated as 25'F, and (730L + 60) is 85'F. Selecting the boltup temperature to be 85'T provides 49'F margin on the current Code requirement based on RTNDT. This margin is appropriato, because boltup is one of the inore limiting 9 operating conditions (high stress and lov teroperature) for brittle fracture.

S 45 D

10CFR50 Appendix G, p a r t g t t.ph IV.A.2, sets minimum temperature requirements for pressure above 20% hydrotest pressure based on the RTNDT Of

)

the closure region. Curve A teinpornturo must be no less than (RTggy + 90'F) and Curve B temperature no less than 'RTypt + 120'F). The Curve A requirement causes a 41'F shift at 20% hydrotest pressure (375 psig) as shown in Figures 41 and 4 2. The curve B requirement has essentially no irepact on the figures because the analytical results for the non-beltline regions require that temperature be greater than 10CFP,50 Appendix 0 requirernent of (RTNDT + 120'F) at 375 psig, 4.5 CORE CRITICAL OPEkATION REQUIREMENTS OF 10CFR50, APTENDIX 0 Curve C, the core critical operation curve shown in Figures 41 and 4 2, is generated from the requirements of 10CFR50 Appendix C, paragraph IV.A.3.

Essentially paragraph IV.A.3 requires that core critical F T limits be 40'T above any Curve A or B limits. Curve B is more limiting than Curve A, so Curve C is Curve B plus 40'F.

Another requirement of IV.A.3, or actually an allowance for the BVR, concerns minimum temperature for initial criticality in a startup. The BVR, given that water level is normal, is allowed initial criticality at the closure flange region (RTNDT + 60'F) at pressures below 375 psig. This requirement makes the minimum criticality temperature 96'F, based on the RTNDT of plate G 307 RI. Above 375 psig, the Curve C temperature must be at least that required for the hydrostatic pressure test (Curve A at 1100 psig). In Figure 4 1, tha non beltline curves are more limiting than this requirement at 375 poig, so there is no impact on the shape of the F T curves. However, in Figure 4 2 there is a step at 375 psig in Curve C due to this requirement.

46

l

) ..

t Table 4-1 i P-T CURVE VALUES FOR 17 ETPY

) .-

Limiting Non-Belt 31ne Curve Curve Temperature (OT) Temp. (OF)

Pressure

[

(psig)_

8- C A A

85.0 85.0 96.0 $5.0

• 0 85.0 85.0 96.0 85.0 10 85.0 85.0 96.0 85.0 20 ,

85.0 85.0 96.0 85.0 i 30 85.0 85.0 85.0 100.0

>- 40 85.0 85.0 113.0 85.0 50 85.0 60 85.0 85.0 124.0 70 85.0 93.5 133.5 85.0 80 85.0 101.7 141.7 85.0 90 85.0 108.7 148.7- 85.0 ,

85.0 114.8 154.8 85.0 100 l 85.0 120.4 160.4 85.0

'110 85.0 120 85.0- 125.3 165.3 85.0 130.1 170.1 85.0 130 85.0 134.7 174.7 85.0 140 85.0 150 85.0 139.0 179.0 85.0 142.9 182.9 85.0 160 186.3 85.0 )

170 85.0 146.3 l 85.0 149.3 189.3 85.0 180

)- '

190 85.0 152.1 192.1 85.0 l

85.0 154.8 194.8 85.0 200 85.0 ,

210. 85.0 157.5 197.5  !

85.0 160.1 200.1 85.0 220 85.0

-230 85.0 162.4 202.4 i 85.0 164.7 204.7 85.0 1 240 85.0 250 85.0 166.9~ 206.9 85.0 169.0- 209.0 85.0 260 85.0 270 85.0 171.0 211.0 1 85.0 173.0 213.0 85.0 1 280- 85.0 290 85.0 174.9 214.9 85.0 176.7 216.7 85.0 300 85.0 310 85.0 178.5 218.5 85.0 180.2 220.2 85.0 .

320 85.0 330 85.0 181.5 221.8 =

k1 340 85.0 183.4 223.4 85.0 85.0 -185.0- 225.0 85.0 350 85.0 360 85.0 186.5- 226.5 228.0 85.0 l 370 85.0 - 188.0 ~

375 85.0. 188.8 228.8 85.0  ;

126.0 188.8 228.8 126.0 375  !

126.0 189.5 229.5 126.0 380

)' -390 126.0 '191.0 231.0 126.0-126.0- 192.5 232.5 126.0 400 126.0 194.0 234.0 126.0 410- 126.0 420 126.0 195.4 235.4 126.0 196.8 236.8 126.0 430 126.0 440 126.0 198.2 238.2 199.5 239.5 126,0 450 f26.0 126.0 200.8 240.8 126.0

,J

'460 126.0 470 126.0 202.1 242.1 126.0 203.3 243.3 126.0 480 k

4 4

) .I Table 4-1 P-T CURVE VAtt1ES FOR 17 ETPY i

Limiting Non-Beltline Curve Curve Pressure ' Temperature (DF) Temp. (DF)

);

(psig)

A B C A 490 126.0 204.5 244.5- 126.0 500 126.0 205.7 245.7 126.0 510 '126.0 206.8- 246.8 126.0

$20 '126.0 207.9 247.9. 126.0

)' 530 126.0 209.0 249.0 126.0 1 540 126.0 210.0 250.0 126.0 550 126.0 '211.0 251.0. 126.0 t 560 '126.0 212.0 252.0 126.0 '

570 126.0- 212.9 252.9 126.0 -

$80 -127.9 213.8 253.8 '127.9 r, $90' 130.1 -214.7 254.7 130.1

[ 600 132.3 215.5 ;255.5 132.3 610 . 134.3 216.3 256.3 134.3 - - -

620 136.3 217.1 257.1 136.3 630- '138.3 217.8 257.8 138.3

{- '

640 140.2' 219.0 259.0- 140.2 r 650 142.0 220.3 260.3 142.0 - 4

=

-660 143.8 221.5 261.5 143.8

), 670 145.6' 222.8. 262.8- 145.6 680

• 147.3 224.0 264.0 147.3 690 149.0 225.2. 265.2 149.0 v 700 226.4 , 266.4 150.6 4 710

[ 150.6 152.2 227.6 267.6 152.2 7 720 154.3' 228.7 268.7 153.7  !

730 156.7 229.8 269.8 .155.2 N 740 159.1 230.9 270.9' 156.7 b 750 161.4 232.0 272.0 2 73.1 138.2 159.6 760 163.6 233.1

-770 165.8':234.2 274'2

. 161.0-780 167.9 235.2 275.2 162.3 790 169.9 236.2 276.2 163.7 i 800 '171.9 237.'l. 277.2 165.0 810- 1 73.8 .238.2- 278.2' 166.3 -

) - 820 175.6 239.2 279.2 167.6 3 830 177.4 240.2 280.2 168.8 -j' 840 .179.2 241.1 281.1 .170.0 850 180.9 242.1 282.1 171.2 l 860s 182.6 243.0 283.0 172.4 '

870- 184.2 243.9 283.9 173.5 <

880- T' 244.8 284.8. 174.7 .

890 ., ', 245.7 285.7 175.8 '

yE .1bo.9 246.6 286.6 176.9

-900 910. 190.4- 247.5_ 287.5 178.0 920 191.9 248.3 288.3 179.0 930: -193.3- 249.2 '289.2 180.1

=940 194.7 250.0- 290.0' 181.1 ~

196.1. 250.8' 290.8 182.2 950 960 197.5 251.6- 291.6- 183.2

)- 970 198.8 252.5 292.5 184.1 980 200.1 253.3' 293.3 185.1 990 201.4 - 254'.0 294.0 186.1 i

'4-8

)]

. _._ j

4 Table 4-1 P-7 CURVE VA14!ES TOR 17 ETPY l

Littiting Non-teltline Curve Curve

' Pressure h nperature (07) Temp. (OT)

(pstr)

A B C A 1000 202.6 254.8 294.8 187.0 1010 203.9 255.6 295.6 10.B . 0 1020 205.1 256.4 296.4 iBB.9

> 1030 206.3 257.1 297.1 189.B 1040 207.4 257.9 297.9 190.7 1050 208.6 258.6 29B.6 191.6 1060 209.7 259.3 299.3 192.5 1070 210.8 260.1 300.1 193.3 1080 211.9 260.8 300.B 194.2 1090 213.0 261.5 301.5 195.0 p 1100 214,0 262.2 302.2 195.B 1110 215.1 262.9 302.9 196.7 1120 216.1 263.6 303.6 197.5 L

1130 217.1 264.2 3 04.2 198.3

, 1140 218.1 264.9 304.9 199.1 1150 219.1 265.6 305.6 199.9 1160 220.1 266.2 306.2 200.6 g 1170 221.0 266.9 306.9 201.4 11B0 222.0 267.6 307.6 202.2 1190 , 222.9 268.2 308.2 202.9 1200 223.8 268.B 300.8 203.7 1210 224.7 269.5 309.5 204.4 1220 225.6 270.1 310.1 205.1 1230 226.5 270.7 310.7 205.B 1240 227.4 271.3 311.3 206.5

> 1250 228.3 271.9 311.9 207.2 1260 229.1 272.5 312.5 207.9 1270 229.9 273.1 313.1 20E.6 1200 230.B 2 73.7 313.7 209.3 1290 231.6 274.3 314.3 210.0 '

1300 232.4 274.9 314.9 210.7 1310 233.2 275.5 315.5 211.3

> 1320 234.0 276.0 316.0 212.0 1330 234.8 276.6 316.6 212.6 1340 235.6 277.2 317.2 213.3 1350 236.3 277.7 317.7 213.9 1360 237.1 278.3 318.3 214.5 1370 237.0 278 B 318.0 215.2 1380 238.6 279.4. 319.4 215.0 y 1390 239.3 279.9 319.9 216.4 1400 240.0 280.5 320.5 217.0 i

4-9

b .

Table 4-2 P-T CURVE VALUES FOR 32 ETTY D

Limiting Non-Beltline Curve Curve D Temp. (or)

Pressure Temperature (DF)

(psir)

A B C A 25.0 85.0 96.0 e5.0 1 0

to 85.0 85.0 96.0 25.0 20 85.0 B5.0 96.0 ,85.0 D 85.0 30 25.0 25.0 96.0 40 25.0 25.0 100.0 85.0 50 E5.0 25.0 113.0 t$.0 60 25.0 25.0 124.0 B5.0 70 85.0 93.5 133.5 25.0 80 85.0 101.7 141.7 85.0 90 85.0 108.7 148.7 B5.0 .

p 114.8 154.8 85.0 100 B5.0 110 25.0 120.4 160.4 85.0 120 85.0 125.3 165.3 B5.0 130 B5.0 130.1 170.1 85.0

\ 140 150 B5.0 85.0 134.7 139.0 174.7 179.0 25.0 B5.0 160 85.0 142.9 182.9 65.0 g 170 85.0 146.3 iS6.3 85.0 1B0 B5.0 149.3 129.3 B5.0 190 85.0 152.1 192.1 85.0 200 B5.0 154.8 194.8 B5.0 210 t$ 0 157.5 197.5 85.0 220 85.0 160,1 200.1 25.0 230 85.0 162.4 202.4 25.0 D 240 E5.0 164.7 204.7 B5.0 250 05.0 166.9 206.9 B5.0 260 85.0 169.0 209.0 85.0 270 85.0 171.0 211.0 85.0 280 85.0 173.0 213.0 85.0 290 85.0 174.9 214.9 05.0 300 85.0 176.7 216.7 E5.0 310 B5.0 17B.5 218.5 85.0 3 320 E5.0 180.2 220.2 B5.0 330 E5.0 181.8 221.6 85.0 340 E5.0 183.4 223.4 B5.0 350 85.0 185.0 225.0 85.0 360 85.0 186.5 226.5 B5.0 370 B5.0 iBB.O 228.0 85.0 375 E5.0 iBB.B 228.6 B5.0 0 375 126.0 188.B 234.0 126.0 380 126.0 189.9 234.0 126.0 390 126.0 192.5 234 0 126.0 400 126.0 197.2 237.2 126.0 410 126.0 199.6 239.6 126.0 420 126.0 201.8 241.B 126.0 430 12 6.0 204.0 244.0 126.0 440 126.0 206.2 246,2 126.0 D

450 126.0 208.2 248.2 126.0 460 126.0 210.2 250.2 126.0 470 126.0 212.2 252.2 126.0 4B0 126.0 214.1 254.1 126.0 0 4-10

l O .

Tatte 4-2 F-T CURVE VALUES FOR 32 ETPY ..

O'- i timitins Non-Seltline O Curve Curve Tetnperatute (OT) Ternp . (OT)

Pressure (psig)_

A 8 C A 490 126.0 215.9 255.9 126.0 500 126.0 217.7 257.7 126.0 0 510 126.0 219.5 259.5 126.0 520 126.0 221.2 261.2 126.0

$30 126.0 222.9 262.9 126.0

$40 126.0 224.5 2 64.5 126.0 550 126.0 226.1 266.1 126.0 560 126.0 227.7 267.7 126.0

~

570 126.0 229.2 269.2 126.0 O, $80 127.9 230.7 270.7 127.9 590 130.3 232.1 272.1 130.1 600 134.8 233.6- 273.6 132.3 610 139.1 234.9 274.9 134.3

\. .

620 143.2 236.3 276.3 277.7 136.3 138.3 630 147.0 237.7 640 150.6 239.0 279.0 140.2 ,

650 154.1 240.3 280.3 142.0 O. -

660 157.3 241.5 281.5. 143.8 670 160.5 242.8 282.8 145.6 163.5 244,0 _ 284.0 147.3 680 690 166.3 245.2 285.2 149.0 700 169.1 2r.6.4 - 286.4- 150.6 710 171.7 247.6 287.6 152.2 720 174.3- 2'B.7 288.7 153.7

.O - 730 176.7 249.8 289.8 155.2 740- 179.1 250.9 -290.9 156.7 750 181.4 252.0 292.0 158.2 760 183.6 253.1 293.1 159.6 770 185.8 254.2 294.2 161.0 780 187.9 255.2' 295.2 162.3 -

790 189.9 256.2 296.2 163.7 O 800 191.9 257.2 297.2 165.0 166.3 )

810 193.8 25B.2 298.2-820 195.6 259.2 299.2 167.6 830 197.4 260.2 300.2 168.8 170,0 840 199.21 261.1- 301.1 850 200.9 262.1 '302.1 171.2 202.6 263.0 303.0 172.4 860-303.9 - 173.5

0. -

870_

880 204.2 205.8 263.9 264.8 304.8 174.7 890 207.4 265.7 305.7- 175.8 900 208.9 266.6 306.6 176.9 910 210.4 267.5 307.5 178.0 920 '211.9 268.3 308.3 179.0 213.3 269.2 309.2 180.1 930 9'O 21'.7 270.0 310.0 181.1

O 950 216.1 270.8 310.8 182.2 960 217.5 271.6 311.6 183.2 970 218.8' 272.5 -312.5 184.1 220.1 273.3 313.3 185.1 980 990 -221.4 274.0 314.0 186.1 4-u 0-

h- .

I Table 4-2 l

P-T CURVE VALUES TOR 32 EFFY Litniting Non-Eeltline Curve Curve Pressure Ternperature (OF) Temp. (O F)

(p r.i g)

A B C A 1000 222.6 274.8 314.8 187.0 1010 223.9 2 75.6 315.6 12.8.0 1020 225.1 276.4 316.4 168.9

> 1030 226.3 2 77.1 317.1 189.8 1040 227.4 277.9 317.9 190.7 1050 228.6 278.6 318.6 191.6 1060 229.7 279.3 319.3 192.5 1070 230.8 280.1 320.1 193.3 1080 231.9 280.8 320.8 194.2 1090 233.0 281.5 321.5 195.0

> 1100 234.0 282.2 322.2 195.8 1110 235.1 282.9 322.9 196.7 1120 236.1 283.6 323.6 197.5 1130 237.1 284.2 324.2 198.3

\ 1140 1150 238.1 239.1 284.9 285.6 324.9 325.6 199.1 199.9 1160 240.1 286.2 326.2 200.6 g 1170 241.0 286.9 326.9 201.4 1180 242.0 287.6 327.6 202.2 1190 242.9 288.2 328.2 202.9 1200 243.8 288.8 328.8 203 7 1210 244.7 289.5 329.5 204.4 1220 245.6 290.1 330.1 205.1 1230 246.5 290.7 330,7 205.8 1240 247.4 291.3 331.3 206.5

> 1250 248.3 291.9 331.9 207.2 1260 249.1 292.5 332.5 207.9 1270 249.9 293.1 333.1 408.6 1280 250.8 293.7 333.7 209.3 1290 251.6 294.3 334.3 *10.0 1300 252.4 294.9 334.9 210.7 1310 '253.2 295.5 335.5 211.3

> 1320 254.0 296.0 336.0 212.0 1330 254.8 296.6 336.6 212.6 1340 255.6 297.2 337.2 213.3 1350 256.3 297.7 337.7 213.9 1360 257.1 298.3 338.3 214.5 1370 257.8 298.8 338.8 215.2 1380 258.6 299.4 339.4 215.8 g 1390 259.3 299.9 339.9 216.4 1400 260.0 300.5 340.5 217.0 g 4-12

l

.o-

, . l

\

.O 1600 i IO A 1400~ ~

f t

DISCONTINUITY LIMITS, 8

^ -

Rindt = 66'f. j- - - --

.[

O BWR/6 CRD CURVE %,e S 1200 - Y- - - --

O f L

6, ,

o e  ! N -.

r 1000 ,r y

• _J #

_ _\._ .\

m . N CORE BELTLINE LIMITS O 800 -,/- ---

wiTH ART or 13e+r e

O FOR LOWER SHELL o __

PLATE C-B-6 6% A - SYSTEM HYDROTEST LIMIT

-O g 600 WlTH FUEL IN VESSEL g B - NON-NUCLEAR HEATUP/

COOLDOWN LIMIT 3 I

_3 C - NUCLEAR (CORE CRITICAL) s - LIMIT g

• "

• DISCONTINUITY LIMITS.

"O m RTndt = 60'F, g --

BWR/6 FW CURVE

' CURVES AB,0 ARE VALD 200 - ~~~

FOR 17 EFPY OF OPERATION BotTup g' co'r p MINIMUM CRITICALITY d p # TEMPERATURE = 56*F O -

0 100 200 300 400 500 600

'O MINIMUM REACTOR VESSEL MET AL TEMPERATURE (*F) -

Figure 4-1. Oyster Creek P-T Curve Valid to 17 EFPY

.. 4-13

D 9

1600  !

D A

'd -

1400 D!SCONTINUITY LIWTS, I

^ -

Rindt 0(?r, j - -~. -

g -[c1 BWR/0 CRD CURVE yl le I v -

1200 1-O (

y [.._,_,_ _ _

CL e' N E '

R 1000 J I

,e- *lx ,

to Ln 4_

e

_N-0 b '

! bg CORE BELTUNE LIMITS g y 800 l-- --

wtTH ART Or 158'r O / FOR LOWER SHELL C f_ _

PLATE G-8-0 L 8 A - SYSTEM HYDROTEST UMIT 1

g 600 -- [- - -

W11H FUEL IN VESSEL B - NON-NUCLEAR HEATUP/

D r C00LDOWN UMiT ,

5 -- --

C - NUCLEAR (CORE CRITICAL)

D UMit E 400 - -

-- - CURVES AfiC ARE VALD

• "

• FOR 32 EFPY OF OPERATION l

y ~~

-I APP G REQU REMENT BASED i i C' N N ON CURVE A c 1100 PS10 200 -- -+

BDLTUP + -- ~ + IN- - D:SCONTINUl[f ,f UMTS, geg j Rindt a 60 BWR/0 FW CURVE g . . _

-. - M:NIMUM CRITICALITY

-" TEMPfR ATURE = 96'F 0 -

j i i 0 100 200 30D 400 500 600 y MIN! MUM REACTOR VESSEL METAL TEMPERATURE (*F)

Figure 4-2 Oyster Creek D-7 Curve Volid to 32 EFPY l

4-14 S

l r r r r r

0 r r re a

2

a t i y =

, T, w r, y d e

r o

/.;,

t i

n o

M g

w d

a e

ri n ey t ur o E Hl e ai t r n VI aENO T

mar t

e p o C,Z An to a mM t p Q -

oe BS ed T a e

w s \g t

) sH b e Tm eo r t uo s

t sB w er e Pt a r

f o ap ee sS r

a w

F F r ro r r

- Cm 0 2 l o 2 2 2 m arf

=

y

=

= = d c n

i e

T, w T, yw r o

t hi eo t t t s o c

/

i nt p u

, \ Mmoi i

L yd H R e

/ d ae en 3 w

Hil t -

E l

e 4 nae T

CuO N

t mB o

t h e

r u

A rZ oit g Bw i

/ F

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' a I \

,1*

f\\lll l 1fl l l , '

4 9

V

.A I

sn s 4

h o M i 4

) o a

O_.

o: o , u O O D i o

L D

1 a I . u I

O C 0-

- E laJ O

{ o D'- W

- a g c.

D N., '- ...

W :e m 2 0 W .d CD A .. ., g w_

w

• O

> Si .

• C e o K 0 %..._ .s

=

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v-I o o o o o o o o o o o o N,-

o e m 5 o h')

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g

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p .?

(qi-u) ADU3N3 .1DVdWI Lu 4-16 5

l

O .

5.0 REFERENCES

O (1) ' Fracture Toughness Requirenents," Appendix C to Part 50 of Title 10 of the Code of Federal Reguladons, July 1983. ,

2) Radiation Embrittlement of Reactor ves. 1 Materials," USNRC Regulatory O Guide 1.99, Revision 2 May 1986.

[3] Hodge, J. M.,

• Properties of Heavy Snetion Nuclear Reactor Steels "

tialding Resear h Council Bulletin 217, July 1976.

O

[4] "Tsicture Toughness Requirements," UFNRC Branch Technical Position ,

MTEL D 2, Revision 1 July 1981.

O

($) MlT er, R. L., " Testing and Evaluation or Irradiated Reactor Vessel Materials Surveillance Program Specimene," GPU Nuclear TDR 725, Revision 3 (to be published).

O ,vanhan et, al. , " Examination, Testing and Evaluad t 1 of Specimens from (6) the an' Irradiated Pressure Vessel Surve111ance Cape 4 for the Oyster

(

C 'eek A riear Generating Station " Battelle Columb..a iA ntories Report ' .

BCL.382 1 %1, Revision 1, October 1985.

(7} " Fracture Toughness Criteria for Prot 9ction Against Failure," Appendix G )

to Section XI of tht. ASME Boiler 6 Pressure Vessel Cade, 1989 Edition v".th 1989 Addenda.

. { 2)

?VRC P9 commendations on Toughness Requirements for Ferritic Materials,"

Ucit.'eg Research Council Bulletin 175. August 1972.

O

[9) Pierson rc. al.,

• Analytical Report for Jersey Central Reactor Vessel,"

Combustion Ing'oeering Report CENC 1143.

O 51

[O>

O '.

APPENDIX A CHARPY CURVES OF SELECTED VESSEL PLATES O.

In order to-establish an appropriate, conservative RTNDT for the beltline plates and several other plates with low USE values, the Charpy data f r e8ch Pl ate were curve fit with a hyperbolic tangent relationship:

O ENERGY = A + B tanh ;(T To)/C) where A, a,.T and C are constants determined by statistically fitting the O.

Chr.rpy data to minimize variance, i

Once the curve t'i t for each material was established, the standard e

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APPENDIX B BELTLINE P T CURVE CALCULATION METHOD 0

The beltline is the region of the vessel that will accumulate more than 1017 n/cm2 fluence during operation. The vessel wall from the bottom of active fuel to the top of active fuel meets these conditions. The Oyster 0- Creek vessel beltline consists of two shells of plates and the connecting volds. Therefore, there are no discontinuity regions to consider in the beltline curve analyses. The methods used for the pressure test and heatup/cooldown curves are described below. The core critical operation curve O is simply the heatup/cooldown curve plus 40'F, as required in 10CFR50 Appendix 0 (1), so the methods for the heatup/cooldown curves t.pply to the core critical curves as well.

O B.1 PRESSURE TEST In general, the methods of ASME Code Section III, Appendix G [7] are used to calculate the pressure test beltline limits. The vessel shell, with

.an inside radius (R) to minimum thickness (tmin) ratio of 15, is treated as a thin walled cylinder, The maximum stress is the hoop stress, given as am - PR/tmin' O The stress intensity factor, Kim, is calculated using Figure G 2214 1 of

(-7), accounting for the proper ratio of stress to yield strength.

Figure G 2214-1 was taken from Welding Research Council (VRC) Bulletin 175 (B), and is based on a 1/4 T radial flaw with a six-co-one aspect ratio-0 (length of 1.5 T) . The flaw is oriented normal to the maximum stress, in this case a vertically oriented flaw. This orientation is used even in the case where the circumferential weld is the limiting beltline material, as mandated by the NRC in the past.

O O

1 B1 I

... .- . - .. . .. ~ . . - . - . . - . .. . . . . ~ -~ ~

O; Pressure test KIR.is the -calculated value KI m. multiplied by a safety g g factor of 1.5, per (7). The relationship.between KIR and temperature relative

- to-reference-temperature (T RTNDT) is shown in Figure G 2210 1 of-[7),. I represented by the relationship g- _KIR 26,78 - 1,233 e [ 0,0145 ( T RTNDT + 160 )l- (B 1)

This relationship is derived in (8) as the lower bound of all dynamic fracture toughness'and crack arrest toughness data. This relationship provides values ,.

LO- ' f Pr*88"r8 (fr m KIR) versus T (from (T RTNDT))'

B2 HEATUP/COOLDOWN

. O;-

The beltline curves for heatup/cooldown conditions are influenced by pressure stresses and thermal stresses, according to the relationship in [7]

KIR - 2,0'K I,+ Kye, (B 2)

.O-e ,!

where KI m.is primary membrane K due to pressure and KI e is radial-thermal gradient K due to

'heatup/cooldown,

~y

-The pressure stress intensity factor K m I is calculated by the method described

. in; section - B',1, the only difference being -the - larger -safety factor applied.

The thermal gradient stress intensity factor calculation is described below.

O The thermal: stresses in the vessel wall -are caused by a radial: thermal gradientiwhich is created by changee in the adj acent reactor coolant  !

temperature in heatup or cooldown conditions. The stress intensity factor is computed by multiplying the coefficient Me from Figure 0-2214-2 of [7] by the through wall temperature gradient ATw. given that the te rature gradient has

^

a through wall shape similar to that shown in Figure G 2214 3 of'[7),

O:

B-2

< O--

The relationship used to compute through wall ATw is based on one dimensional heat conduction through an insulated flat plate:

62T(x,t)/6x2 - 1/S (6T(x,t)/6t), where (B 3) f(x,t) is temperature of the plate at depth x and time t D

is thermal diffusivity (ft 2/hr),

Maximut stress will occur when the radici thermal gradient reaches a quasi steady state distribution, so that 6T(x,t)/6t - dT(t)/dt - G, where G is D

the heatup/cooldown rate, in this case 100*F/hr. The differential equation is integrated over x for the following boundary conditions, shown in Figure B 1:

1. Vessel inside surface (x - 0) temperature is the same as the coolant D

temperature, To,

2. Vessel outside surface (x - C) is perfectly insulated, so the thermal gradient dT/dx - 0.

D The integrated solution results in the following relationship for wall temperature:

D T - Cx2/2 GCx/p + To (B 4)

This equation is normalized to plot (T - To)/ATw versus x/C in Figure B 2.

The resulting through-wall gradient compares very closely with Figure G 2214 3 D Therefore, ATw calculated from Equation B-4 is used with the of (7).

appropriate Mt of Figure G 2214-2 of (7) to compute kit for heatup and cooldown.

D The Me relationships were derived in (8) for infinitely long cracks of 1/4 T and 1/8 T. For the flat plate geometry and radial thermal gradient, orientation of the crack is not important.

D B3 D

The stress generated by the thermal gradient is a bending stress that changes sign from one side of the plate to the other. In combining pressure

) and thermal stresses, it is usually necessary to evaluate stresses at the 1/4 T location (inside surface flaw) and the 3/4 T location (outside surface flaw). This is because the thermal gradient tensile stress of interest is in the inner wall during cooldown and is in the outer wall during heatup.

) However, as a conservative simplification, the thermal gradient stress at the 1/4 T is assumed to be tensile for both heatup and cooldown. This results in the conservative approach of applying the maximum tensile stress at the 1/4 T location. This approach is conservative because irradiation effects cause the f allowable-toughness, KIR, at 1/4 T to be less than that at 3/4 T for a given metal temperature. This conservatism of the approach causes no operation difficulties, since the BWR is at steam saturation conditions during normal heatup or cooldown, well above the heatu,/cooldown curve limits.

B.3 EXAMPLE CALCUIATION 17 EFPY PRESSURE TEST AT 1000 PSIG The following inputs were used in the beltline limit calculation:

ART ........................... 138'F Vessel Height .................. 766 inch Bottom of Active Fuel Height .. 209.3 inch

) Vessel Radius .................. 106.7 inch Vessel Thickness .............. 7.125 inch Beltline Material Sy ........ 62.7 ksi

) Pressure was calculated to include hydrostatic pressure for a full vessel:

P - 1000 psi + (766 209.3) inch

• 0.0361 psi / inch - 1020.1 usig

) Pressure stress:

o - PR/t - 1020.1 psig

• 106.7 inch / 7.125 inch - 15276 osi

)

B-4

)

t

Ol

-The-factor.M. depends'on (a/S y ) and /t:-

.O

~

-o/Sy - 15276 / 62700 - 0,24 (use a/Sy - 0.5)

. /t - (7.125)l/2 -.l2.67 O- Mm - 2.d1 The stress intensity factor, K m, i is Mm

• 0:

QL KI m - 2.57

• 15276 - 39259 psi /in - 39.3 ksilin Equation.(B 1) can be rearranged, and 1.5*K I m substituted for KIR. to 80lVC l' for (T RTNDT):-

O-(T - RTNDT) - in[(1.5*K Im 26.78)/1,233]/0.0145 -160

._(T RTNDT) - In((1.5*39.3 26.78)/1.233]/0,0145 - 160

(T - RTNDT) " M '

0 :- 3 Adding the adjusted RTNDT for 17 EFPY ofl13B'F:

T - 203*F of

B ,4.:- . EXAMPLE CALCULATION. - 17_ EFPY llEATUP/C00LD0k'N -CURVE AT :1000 PSIC -

O

-The-heatup/cooldown curve at-1000 psig uses-the same KI m as the pressure-

-- test curve,-but with a safety factor-of'2.0-instead of;1.5. -In addition, there.is;a kit- term for"the_ thermal stress. The additional inputs .used to O  : calculate-kit.are:

-G - 100'F/hr' C_- 7.34 inches, including clad thickness

.O 1 4.- 0 354 te2/hr at 550*F (most conservative-value)

O-B5

Equation'B.4 canbe solved'for the through. wall-temperature (x-C),

resulting in the: absolute value of AT for heatup or cooldown of' AT~- 002/2$-

For the values above, AT - 52.8'F.

The analyzed: case for thermal stress is a 1/4 T flaw depth with 111 thickness-of 7.34 1.iches. From ASME Appendix C Figure 0 2214 2, the

.; -corresponding'value of Mg is Me - M

Thus-the thermal' stress intensity factor, Kit Me

• AT, is calculated to be Kit - 16.9'ksilin  :!

The pressure land thermal stress terms are-. substituted-into Equation B 1 to.  ;

)

solve for'(T-.-RTNOT):

_(T. RTNDT) - In[((2.0*39.2 + 16.9) . 26.78)/1.233]/0.0145 160 (T - RTNDT) - 117'F

Adding the adjusted _ RTNDT for 17 EFPY of 138'F

q

)

T -'255'F p

q B6

Lo '

i l

0 f

N O

Reactor Coolant

• Cooldown Rate O G=100 F/hr e77ex=o

\nsulation l

O T=To N

O Inside Outside Surface Surface O \

e x

x=0 x=C O

O Figure B- 1. Boundary Conditions for Heatup/Cooldown Temperature O

O

Q 4

0:

0 100 p O 90

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it

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.: /

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ic 50 f

i 6 40 /

0 . /

5 15 30

/

/

--g 10 ,

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0--

0 20. 40 60 80 100 W0ll Thickness, %

0 0

Figure : 6-2. Assumed Through-Wall Temperature During-Heatup/Cooldown O

O-I

C  ;

h, 6

APPENDIX C IMPACT ON P T CURVES OF HEATUP/COOLDOW RATE Civen the form of the equation by which ATy is determined, the heatup/cooldown rate of 100*F/hr for brittle fracture purposes refers to an instantaneous rate. Instantaneous rates in excess of 100'F/hr are allowed for D

in the Technical Specification, as long as a temperature change of 100*F in a one hour period is not exceeded. This is based on the fact that the 1/4 T location of the assumed flaw sees little if any effect of small perturbations in the 100'F/hr rrite, due to the thermal inertia of the vessel wall. It is D

understood in this Tech Spec allowance that operators will track vessel coolant heatup or cooldown to stay as close to a 100'F/hr rate as possible.

The method of calculating K7t in Appendix B can be used to D While conservatively adjust the P-T curves for higher heatup/cooldown rates.

it is expected that short periods of excessive rates will not affect the 1/4 T location, a conservative approach in to increase the thermal K proportionally to the increased rate. Thus, for a 200'F/hr heatup or cooldown, Kit would D

double.

The calculation of beltline P T limits was modified to include a 200*F/hr heatup/cooldown rate. The resulting P-T curve for 17 EFPY of D

operacion is shown in Figure C 1. The non beltline limtts are not char.ged because they are based on more severe transient conditions at the discontinuities. In cases where the vessel coolant instantaneous heatup or cooldown rate, as measured by the steam dome pressure, exceeds 100'F/hr but is D

less than 200'F/hr, Figure C1 can be used to assure that vessel PT requirements have not been exceeded.

D D

C1 1 D l

0

). ,4 e

1600 A

arco n'A B C 1400 l-t DISCONilNUITY LIMITS, 8 g

^ -

Rindt = 66*F, -l- -- =

.[ BWR/6 CRD CURVE % l 3 1200 - I- -- --

a  ;

b7

$ e e' \~ s -

r 1000 N J l x W .' s N LA 8 N

' CORE BELTLINE LtMITS g ,

g 800 - s .

wlTH ART OF 13Sor O FOR LOWER SHELL

$ PLATE G-8-6 b% A - SYSTEM HYDROTEST LIMIT p z 600 -- ---

WITH FUEL IN VESSEL g 8 - NON-NUCLEAR HEATUP/

g _ _

COOLDOWN LIMIT

--) C - NUCLEAR (CORE CRITICAL)

LNii m 400 g a 375 esic jf M / CURVE 3 AB.C ARE VAUD E FOR 17 EFPY OF OPERATION CL (CURVES B AND C INCLUDE 200 -

200'F/m t-EATUP/COOLDOWN)

DOLTUP

> 85'F y MINIMUM CRITICALITY

/ TEMPERATURE = 148'F 0 -

, i 0 100 200 300 400 500 600 MINIMUM REACTOR VESSEL METAL TEMPERATURE ( f)

Figure C- 1. Oyster Creek P-T Curve Valid to 17 EFPY

.- _ - - _ - _ _ _ _ _ _ _ _ _