Text

Forwards Rev 1 of Util 941214 Response to NRC Rai, ,re 10CFR50.61 Screening Criterion
	ML18064A533
Person / Time
Site:	Palisades
Issue date:	12/28/1994
From:	French R; CONSUMERS ENERGY CO. (FORMERLY CONSUMERS POWER CO.)
To:	; NRC OFFICE OF INFORMATION RESOURCES MANAGEMENT (IRM)
References
	TAC-M83227, NUDOCS 9501050020
	Download: ML18064A533 (150)
	v • d • e

)

-1 consumers Power POW ERi Nii ll/llCHlliAN'S PROliRESS Site Offices: 27780 Blue Star Memorial Highway, Covert Ml 49043 * (616) 764-8913, Ext 0210 December 28, 1994 Nuclear Regulatory Commission Document Control Desk Washington, DC 20555 DOCKET 50-255 - LICENSE DPR PALISADES PLANT Robert A Fenech Vice President Nuclear Operations RESPONSE TO REQUEST FOR ADDITIONAL INFORMATION, REVISION 1 - 10CFR50.61 SCREENING CRITERION (RE: TAC NO. M83227)

This is Revision 1 of our December 14, 1994 response (Revision 0) to the NRC request for Additional Information (RAI) dated November 30, 1994.

As requested by the RAI, Revision 0 submitted available data. It also provided analysis and evaluation results which were available at that time.

Revision 1 supersedes Revision O and provides: (1) changes to some of the data provided in revision O; and, (2) the results of our analyses and evaluations.

Consumers Power Company (CPC) letters submitted November 8, 10 and 18 provided information that summarized the results of tests performed on weld material from the retired Palisades steam generators. In our November 18,1994 letter, we also committed to submit, before March 1, 1995, a site specific surveillance plan for staff approval.

For the integrated portion of this plan that involv~s use of credible data from other plants, we have accelerated our schedule to now have an integrated surveillance plan, which addresses the Heat No. W5214 weld material, submitted by the end of January 1995. Credible W5214 weld material data exists for Indian Point 2, Indian Point 3, and H.B. Robinson 2.

The submittal will address the credibility of W5214 data from these plants for use by Palisades.

Use of credible*surveillance data can provide extra operating margin to the PTS screening criteria limit due to a reduced Margin Term as defined in Position 2.1 of Regulatory Guide 1.99 Revision 2.

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2 The tests on weld material from our retired steam generators were initiated and performed by CPC to increase the size of; and thus increase the accuracy of, the industry database for weld material fabricated using weld wire from Heat Nos.

W5214 and 34B009.

Additionally, since this material is in both the retired Palisades steam generators and the active Palisades reactor vessel, the tests were initiated to determine if material from the retired steam generators is suitable for use in a supplemental surveillance program as a surrogate for reactor vessel material. This test program is ongoing.

The NRC RAI dated November 30, 1994 requested six items of additional information to enable the staff to complete their review on this subject. The information requested by the November 30, 1994 RAI was further clarified during a telephone discussion with the staff -0n December 6, 1994.

As a result of that discussion we are including, as Attachment 7 to this submittal, our preliminary plans for further testing of weld material from our retired steam generators.

This Revision 1 provides our complete response.

The following are the six items of information reqtiested and our response to each.

NRC RAI Item No. 1 "Provide the actual time {above 500"F), temperatures, and cooling method for stress relief of the Palisades reactor vessel axial beltline welds and the Palisades stea/11 generators.

Assess the potential effects any difference in the heat treatment could have on the unirradiated reference temperature of the steam generator and the reactor vessel beltline welds."

CPC Response In order to determine the time at temperature for each component during the interstage and final Post Weld Heat Treatment (PWHT), ABB has reviewed the furnace logs and thermocouple strip charts to determine the data requested.

This is shown in Attachment 1.

Differences in heat treatment have not been determined to have any significant effect on the reference temperature of the unirradiated steam generator and reactor vessel beltline welds. This is further discussed in Attachment No.

1.

Ongoing work with AEA. may better assess whether differences in the heat treatment had any effect on the steam generator material.

NRC RAI Item No. 2

'Compare the Charpy and drop weight data from the steam generators to the CE generic weld data base. Provide any data that demonstrates the variability of the nil ductility transition temperature (NOTT) and unirradiated reference temperature in a weld or within a heat of weld wire."

3 CPC Response The Charpy and drop weight data from the steam generator weld samples have been compared to the CE generic weld data base (CEN-189 data). Available data that demonstrates typical variability of the drop weight nil-ductility transition temperature (NOTT) and the unirradiated reference temperature (RTNor) for a specific heat of weld wire are provided by ABB Combustion Engineering Nuc 1 ear Operations (ABB CENO) in Attachment 2.

Further supporting information is provided by ATI Consulting in Attachment 2A.

In summary, when there are two test results for welds fabricated usi_ng weld wire from the same heat, the NOTT and the RTNor temperatures are found to vary l0°F to 30°F between results.

The differences in the initial RTNor values between the Palisades steam generator W5214 data and the earlier generic data base on similar welds may be considered to be within the normal range of variation for these types of materials.

However, sufficient uncertainty exists relative to the condition of the steam generator W5214 material which prevents it from being considered as being specifically representative of the initial baseline properties of the reactor vessel weld seams.

In particular, the measured initial RTNo~ for the steam generator weld material was great~r than two standard deviations from the generic -S6°F value.

The response to Item No. 3 below supports the fact that the steam generator Heat No. W5214 weld material Charpy test results vary significantly from the results obtained from other sample material in the Heat No. W5214 Charpy test data base.

Therefore, it is appropriate to continue to use the generic mean value of -S6°F for the reactor vessel W5214 welds.

NRC RAJ Item No. 3 "Provide a rigorous statistical evaluation of steam generator Charpy data to determine whether the data is statistically equivalent to the surveillance data from (a) the Indian Point-2 surveillance weld, (b) the Indian Point-3 surveillance weld, (c) the Robinson 2 surveillance weld, and (d) a77 three surveillance welds."

CPC Response The requested evaluation has been completed for CPC by ATI Consulting and is included as Attachment 3. Overall, Attachment 3 shows that at an approximate 90% probability 1eve1, the Pa 1 i sades steam generator Charpy data is different than any of the other Charpy data from reactor pressure vessel surveillance programs for weld wire Heat No.

W5214.

. NRC RAI Item No. 4 "Provide unaged and aged Charpy data from the material therma17y aged in the Palisades reactor vessel. What is its percent copper, nickel and phosphorus?

Proyide its neutron flux and fluence, if its irradiation exceeded 1£16 n/cm2 (>lMeV).

Provide the time and temperature hi~tory of the Palisades reactor vessel at normal operating temperatures with the core critical. Provide the operating temperature and the total time at operating temperature for the welds in the steam generators."

CPC Response 4

The unaged Charpy results for the material in the Palisades surveillance program are listed in Tables 3 through 6 from "Final Report on Palisades Pressure Vessel Irradiation Surveillance Program: Unirradiated Mechanical Properties to Consumers Power", Perrin and Fromm, August 25, 1977. They are included in Attachment No. 4 to this submittal as Tables 4-1 through 4-4.

Aged Charpy results are described in Tables 5-2 through 5-9 in Westinghouse report WCAP-10637, "Analysis of Capsules T-330 and W-290 from the Consumers Power Company Palisades Reactor Vessel Radiati.on Surveillance Program",

Kunka and Cheney, September 1984.

They are included in this submittal as*

Tables 4-5 through 4-12 in Attachment No. 4.

Figures 4-1 through 4-4 in Attachment No. 4 represent comparison plots of the unaged and aged material properties using a hyperbolic tangent curve fitting routine.

Copper, nickel and phosphorus measurements performed on the Pali sades surveillance weld and plate materials are listed in Tables 4-13 and 4-14 in Attachment No. 4.

The thermal capsule did not have dosimetry installed as part of the capsule, therefore there is no measured flux or fluence of the thermally aged material.

However, original design specifications for the thermal capsules calculated that the maximum accumulated dose would not exceed 5.0 x 1013 (n/cm2 ) over 40 years at the center of the capsule.

In-house scoping confirms this and shows that, for the time it resided in the vessel, the bottom portion*of the thermal capsule (weld material) received an approximate accumulated fluence of 4.0 x 1016 (n/cm2 ) or less. The heat affected zone (HAZ) material which was above the center of the capsule had an approximate fluence of 2.0 x 1010 (n/cm2 ) or less.

The operating time and temperatures of the reactor vessel and steam generator welds are shown in Table 4-15 in Attachment No. 4.

The total time at operating temperature for the welds in the steam generators can be estimated as the hours critical plus a small percentage of time to cover hot shutdown conditions.

At this time, the thermal history of the steam generator weld material during Cycles 1 through 8 is not believed to have caused a significan~ change in toughness properties.

An assessment of this is provided in Attachment 1.

Ongoing work with AEA may better assess whether aging had any effect on the steam generator material.

NRC RAI Item No. 5 "Provide the approximate number of cons of weld wire in heat W5214.

Describe (a) the weld samples that make up the W5214 percent copper data base, (b) the locations within the samples where the percent copper was measured, and (c) the number of copper-coated filler coils used in the fabrication of the weld.

Provide the measured percent copper values from each sample and the average value from each sample.

Based on this information and data, provide your best-estimate value of the percent copper for the weld heat W5214 and the basis for the value.

Provide the best-estimate value of the percent phosphorus for welds fabricated with weld heat W5214."

CPC Response All the requested data, including the best estimate values, are provided in Attachment 5.

Note that some data has been revised and additional data has been provided.

The best estimate value of the percent copper for weld wire Heat No.

W5214 has been conservatively determined to be 0.212 which is the mean of the selected data.

The best estimate value of the percent*

phosphorus has been determined to be 0.017 which is also the mean of the selected data.

When the mean value of 0.212 percent copper is used with the previously submitted percent nickel value of 1.02, we estimate that Heat No. W5214 weld material will exceed the 10CFR50.61 screening criteria in April of the year 2000.

We will submit a revised engineering analysis to support this data on or before January 13, 1995.

5 It is worth noting that certain members of the Delphi Group (descr1b~d in Attachment No. 5) are of the opinion that using the median value of the copper content would result in a more representative best estimate.

(Given the fact that the data does not represent a normal distribution made up of a large population of data points, the mean can be significantly affected by a single data point at the boundary of the data base. Therefore the median can be more representative of the best estimate than the mean.)

The median value is 0.19 percent copper; its use would extend the time before Heat No. W5214 weld material would exceed the screening criteria by several years beyond the year 2000.

However, we have decided to continue to conservatively use, as noted above, the mean value as the basis for our estimate.

NRC RAI Item No. 6 "Perform a -statistical evaluation to determine if the copper values from the steam generator welds are from the same population as the copper values from the other W5214 welds.

Discuss the implications of the results of this analysis on your evaluation of the amount of copper in the Palisades reactor vessel beltline welds that were fabricated using heat W5214 weld wire.

CPC Response The requested evaluation was performed by and is discussed by ABB-CENO in Attachment No. 6.

Based on that discussion, we conclude the Palisades steam generator welds are from the same population as the welds from the other Heat No. W5214 weld samples.

The overall implications of the results of this evaluation are provided in our response to RAI Item No. 5.

Attachments No. 1 through No. 6 contain tables, figures and explanatory data which support our responses to RAI Items No. 1 through No. 6.

Attachment No. 7 provides a preliminary description of our plan to further evaluate the weld material from our retired steam generators.

As we committed in our November 18th letter, that plan will be submitted before March 1, 1995.

There is no proprietary information in this submittal.

Summary of Commitments 6

1.

On or before January 13, 1995, submit a revised engineering analysis that supports our estimate that the welds in the Palisades reactor vessel which are fabricated with wire from Heat No. W5214 will exceed the IOCFR50.61 screening criteria in April of year 2000.

Robert A. Fenech Vice President, Nuclear Operations CC Administrator, Region III, USNRC NRC Resident Inspector - Palisades Attachments

ATTACHMENT 1 Consumers Power Company Palisades Plant Docket 50-255 RESPONSE TO NRC NOVEMBER 30,1994 REQUEST FOR ADDITIONAL INFORMATION REVISION 1 10CFR50.61 SCREENING CRITERION ITEM NO. 1 The information in this Attachment was provided by ABB/CE Nuclear Operations (ABB-CENO).

DESCRIPTION OF POST WELD HEAT TREATMENT A general description of the post weld heat treatment (PWHT) requirements for raising and lowering temperature of the components is provided below:

1)

When the weldment is placed in the furnace, the furnace temperature shall not exceed 600°F.

2)

At temperatures above 600°F, the maximum rate at which the temperature of the weldment may be raised shall be the lesser of 400°F per hour, or 400 divided by the maximum shell or head plate thickness in inches, but need not be less than 100°F per hour.

3)

During heating, the temperature difference between any two points on the part of the weldment being heated shall not exceed 250°F within any 15 ft. interval of length. During holding time, the maximum temperature difference between any two points shall not exceed 100°F in the portion of the vessel being heated.

4)

The maximum at which the temperature of the weldment is lowered shall be the lesser of 500°F per hour or 500 divided by the maximum shell or head thickness in inches, but need not be less than 100°F per hour. The weldment may be removed from the furnace or local heating may be stopped when the maximum temperature of the weldment has fallen to 600°F. The cooling rate of P-7 materials will be in accordance with special procedures.

The actual time of temperature has been determined for the reactor vessel and each steam generator.

The temperature and duration was determined by reading actual thermocouple output strip charts. The information in the tables includes the heatup and cooldown cycle for each interstage and final PWHT of these components. A summary table has been compiled to identify the cumulative (interstage and final PWHT) time at temperature for a component.

Post Weld Heat Treatment Times In order to determine the time at temperature for each component during the interstage and final Post Weld Heat Treatment (PWHT),

ABB has reviewed the furnace logs and thermocouple strip charts to determine the data in the attached tables.

The time shown on the attached tables is greater than that reported on previous submittals. The reason for this is that the initial data reported was from the furnace inspection logs which report the "hold" time as required by the applicable weld procedure

or M&P (Material & Process) Specification. The inspectors were trained to interpret the "hold" time on the furnace charts as that time during which all thermocouples for all component in the furnace were within the specified range (i.e. 1100°F-1150°F for 15 minutes). For this reason a thinner component, such as a steam generator shell, in a heat treat with a-thicker reactor vessel shell would reach 1100°F-1150°F first and would remain within that range longer waiting on the temperature of the thicker part to come within the required range. The revised tables reflect the time at temperature information for each component as determined by individual component thermocouple reading.

PALISADES HEAT TREAT

SUMMARY

SHEET 2966 B-1 S.G.

2966 B-2 S.G.

Temperature, °F Hours Minutes Hours Minutes 600-700 25 52 27 10 700-800 38 25 24 14 800-900 59 8

29 41 900-1000 31 54 33 1000-1100 37 2

25 8

1100-1175 24 35 16 28 1175-1200 37 2966A - Reactor Vessel Intermediate Shell Temperature. °F Hours Minutes 600-700 14 25 700-800 15 40 800-900 22 20 900-1000 20 35 1000-1100 17 20 1100-1175 16 15 2966A - Reactor Vessel Lower Shell Temperature, °F Hours Minutes 600-700 15 25 700-800 18 55 800-900 29 0

900-1000 26 20 1000-1100 22 10 1100-1175 18 05 F:IDATAIRVllPALRVl\\296681.SB

CONTRACT 2966 B-2 S.G.

Pg 1of7 COMPONENT Upper Shell Head INT.

x HEAT TREAT# N-89 FINAL DATE 4-11-67 TEMPERATURE Hour

- 1ThtE-Minutes 500-600 25 600-700 20 700-800 30 800-900 45 900-1000 55 1000-1100 2

5 1100-1175 2

25 1175-1200 1100-1000 1

1000-900 1

25 900-800 1

20 800-700 1

40 700-600 600-500 800-900 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 5 min.

900-1000 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 20 min.

1000-1100 TOTAL 3 hours3.472222e-5 days 8.333333e-4 hours 4.960317e-6 weeks 1.1415e-6 months 5 min.

1100-1175 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 25 min.

MAXThU.TM TEMPERATURE 1150 DEGREES FARENHEIT

CONTRACT 2966 B-2 S.G.

Pg 2 of 7 COMPONENT Upper Shell/Cone INT.

x HEAT TREAT# 0-24 FINAL DATE 6-10-67 TE:MPERATURE Hour

- TIME-Minutes 500-600 30 600-700 35 700-800 35 800-900 40 900-1000 35 1000-1100 1

15 1100-1175 35 1175-1200 1100-1000 1

1000-900 1

15 900-800 1

40 800-700 1

50 700-600 2

40 600-500 800-900 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 20 min.

900-1000 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 50 min.

1000-1100 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 15 min.

1100-1175 TOTAL 35 min.

\\-IAXIl\\fUM TEMPERATURE 1150 DEGREES F ARENHEIT

CONTRACT 2966 B-2 S.G.

Pg 3 of 7 COMPONENT Upper Shell/Cone INT.

x HEAT TREAT # 0-63 FINAL DATE 8-19-67 TE:MPERATURE Hour

- TIME-Minutes 500-600 40 600-700.

35 700-800 50 800-900 1

900-1000 1

45 1000-1100 2

5 1100-1175 30 1175-1200 1100-1000 50.

1000-900 1

20 900-800 1

40 800-700 2

5 700-600 2

30 600-500 3

15 800-900 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 40 min.

900-1000 TOTAL 3 hours3.472222e-5 days 8.333333e-4 hours 4.960317e-6 weeks 1.1415e-6 months 5 min.

1000-1100 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 55 min.

1100-1175 TOTAL 30 min.

'.\\lAXIMlJ~l TEMPERATURE 1130 DEGREESFARENHEIT

CONTRACT 2966 B-2 S.G.

Pg 4 of 7 COMPO~'ENT Upper Shell/Cone INT.

x HEAT TREAT # 0 FINAL DATE 9-26-67 TEMPERATURE Hour

-T'E-Minutes 500-600 55 600-700 40 700-800 35 800-900 40 900-1000 1

10 1000-llOO 45 l100-l175 1

5 ll 75-1200 1100-1000 1

5 1000-900 1

20 900-800 1

35 800-700 2

10 700-600 2

30 600-500 800-900 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 15 min.

900-1000 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 30 min.

1000-1100 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 50 min.

1100-1175 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 5 min.

MAXL\\IVM TEMPERATURE 1140 DEGREES F ARENHEIT

CONTRACT 2966 B-2 S.G.

Pg 5 of 7 COMPONENT Upper Shell/Cone INT.

x HEAT TREAT # 0-92 FINAL DATE 10-13-67 TEMPERATURE Hour

- TIME-Minutes 500-600 50 600-700 1

10 700-800 55 800-900 30 900-1000 40 1000-1100 55 1100-1175 1

15 1175-1200 1100-1000 55 1000-900 1

20 900-800 1

45 800-700 1

700-600 600-500 800-900 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 15 min.

900-1000 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 1000-1100 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 50 min.

1100-1175 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 15 min.

MAXTh-IU'M TEMPERATURE 1130 DEGREES FARENHEIT

CONTRACT 2966 B-2 S.G.

Pg 6 of 7

Local Heat Treat COMPONENT Upper Shell/Head INT.

x HEAT TREAT # R-51 FINAL

- DATE 6-11-68 TEMPERATURE Hour

- TIME-Minutes 500-600 25 600-700 45 700-800 1

7 800-900 36 900-1000 45 1000-1100 40 1100-1175 28 1175-1200 1100-1000 33 1000-900 30 900-800 30 800-700 37 700-600 45 600-500 1

800-900 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 6 min.

900-1000 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 15 min.

1000-1100 TOTAL l hour 13 min.

1100-1175 TOTAL.

28 min.

MAXIl\\fUM TEMPERATURE 1150 DEGREES FARENHEIT

Local heat treat would a l onl pp y Q.ll!Y to the to 5 teet ot the u p

pp er shell assembl.

y

/

CONTRACT 2966 B-2 S.G.

Pg 7 of 7

-. - DA.TE __ 1041-68 500-600 3

600-700 7

700-800 4

40 800-900 5

900-1000 5

1000-1100 5

1100-1175 10 10 1175-1200 1100-1000 7

1000-900 15 900-800 12 800-700 5

40 700-600 7

40 600-500 6

- 800-900

-*-

T

__ *_o_-.* T_Al./ ___ --

17 hours1.967593e-4 days 0.00472 hours 2.810847e-5 weeks 6.4685e-6 months 900-1000 TOTAL*

20 hours2.314815e-4 days 0.00556 hours 3.306878e-5 weeks 7.61e-6 months 1000-1100 TOTAL-12 hours 1100-1175 TOTAL 10 hours1.157407e-4 days 0.00278 hours 1.653439e-5 weeks 3.805e-6 months 10 min.

MAXIMUM TEMPERATURE 1160 DEGREES FARENHEIT

CONTRACT 2966 B-1 S.G.

Pg 1of10 COMPONENT Upper Shell INT.

x HEAT TREAT # N-34 FINAL DATE 12-21-66 TEMPERATURE Hour

- TIME-Minutes 500-600 40 600-700 30 700-800 25 800-900 30 900-1000 40 1000-1100 50 1100-1175 l

1175-1200 1100-1000 45 1000-900 40 900-800 1

800-700 l

700-600 600-500 800-900.

TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 30 min.

900-1000 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 20 min.

1000-1100 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 35 min.

1100-1175 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months MAXIMUM TEMPERATURE 1150 DEGREES F ARENHEIT

CONTRACT 2966 B-1 S.G.

Pg 2 of 10 COMPONENT Upper Shell/Cone INT.

x HEAT TREAT# N-54 FINAL DATE 2-1-67 TE.MPERATURE Hour

- TThlE-Minutes 500-600 30 600-700 50 700-800 1

10 800-900 1

10 900-1000 1

. 50 1000-1100 2

30 1100-1175 1

10 1175-1200 1100-1000 1

20 1000-900 1

40 900-800 2

10 800-700 1

10 700-600 600-500 800-900 TOTAL 3 hours3.472222e-5 days 8.333333e-4 hours 4.960317e-6 weeks 1.1415e-6 months 20 min.

900-1000 TOTAL 3 hours3.472222e-5 days 8.333333e-4 hours 4.960317e-6 weeks 1.1415e-6 months 30 min.

1000-1100 TOTAL 3 hours3.472222e-5 days 8.333333e-4 hours 4.960317e-6 weeks 1.1415e-6 months 50 min.

1100-1175 TOTAL l hour 10 min.

~lAXIMlIM TEMPERATURE 1140 DEGREES F ARENHEIT

CONTRACT 2966 B-1 S.G.

Pg 3 of 10 COMPOl'rENT Upper Shell/Cone INT.

x HEAT TREAT# N-79 FINAL DATE 3-24-67 TEl\\fi>ERA TURE Hour

- TIME-Minutes 500-600 25 600-700 40 700-800 40 800-900 35 900-1000 40 1000-1100 1

10 1100-1175 1

10 1175-1200 1100-1000 50 1000-900 1

10 900-800 1

10 800-700 1

50 700-600 600-500 800-900 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 45 min.

900-1000 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 50 min.

1000-1100 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 1100-1175 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 10 min.

\\lAXIM.U~l TEMPERATURE 1145 DEGREES F ARENHEIT

CONTRACT 2966 B-1 S.G.

Pg 4 of 10 COMPO~'ENT Upper S_hell/Cone INT.

x HEAT TREAT # N-95 FINAL DATE 4-25-67 TEMPERATURE Hour

-TTh1E-Minutes 500-600 20 600-700 30 700-800 l

10 800-900 45 900-1000 l

1000-1100 2

30 1100-1175 l

40 1175-1200 1100-1000 50 1000-900 1

20 900-800 2

800-700 2

30 700-600 45 600-500 800-900 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 45 min.

900-1000 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 20 min.

1000-1100 TOTAL 3 hours3.472222e-5 days 8.333333e-4 hours 4.960317e-6 weeks 1.1415e-6 months 20 min.

1100-1175 TOTAL 1* hour 40 min.

~IA.XL.\\UJ~I TEMPERATURE 1150 DEGREES FARENHEIT

CONTRACT 2966 B-1 S.G.

Pg 5 of 10 COMPONENT Upper Shell/Cone INT.

x HEAT TREAT# 0-7 FINAL DATE 5-13-67 TE:MPERATURE Hour

- TIME-Minutes 500-600 25 600-700 55 700-800 35 800-900 1

15 900-1000 45 1000-1100 1

25 1100-1175 35 1175-1200 1100-1000 40 1000-900 1

900-800 1

15 800-700 1

45 700-600 2

10 600-500 2

35 800-900 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 30 min.

900-1000 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 45 min.

1000-1100 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 5 min.

1100-1175 TOTAL 35 min.

\\ lAXf.\\-IL M TEl\\'iPERA TURE 1130 DEGREES F ARENHEIT

CONTRACT 2966 B-1 S.G.

Pg 6 of 10 COl\\ilPONENT Upper Shell/Cone INT.

x HEAT TREAT# 0-25 FINAL DATE 6-12-67 TEMPERATURE Hour

- TIME-Minutes 500-600 45 600-700 35 700-800 55 800-900 1

900-1000 55 1000-1100 1

20 1100-1175 30 1175-1200 1100-1000 1

1000-900 1

55 900-800 2

800-700 55 700-600 600-500 800-900 TOTAL 3 hours3.472222e-5 days 8.333333e-4 hours 4.960317e-6 weeks 1.1415e-6 months 900-1000 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 50 min.

1000-1100 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 20 min.

1100-1175 TOTAL 30 min.

\\IA.XThlUM TEMPERATURE 1145 DEGREES FARENHEIT

CONTRACT 2966 B-1 S.G.

Pg 7 of 10 COMPONENT Upper Shell/Cone INT.

x HEAT TREAT # 0-37 FINAL DATE 7-2-67 TEMPERATURE Hour

-T'E-Minutes 500-600 35 600-700 45 700-800 55 800-900 1

10 900-1000 35 1000-1100 35 1100-1175 50 1175-1200 1100-1000 1

1000-900 1

30 900-800 1

50 800-700 50 700-600 600-500 800-900 TOTAL 3 hours3.472222e-5 days 8.333333e-4 hours 4.960317e-6 weeks 1.1415e-6 months 900-1000 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 5 min.

1000-1100 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 35 min.

1100-1175 TOTAL 50 min.

\\lAXIMUM TEMPERA Tl.IRE 1150 DEGREES F ARENHEIT

CONTRACT 2966 B-1 S.G.

Local Heat Treat COMPO~ifu'IT Uuugr Shell/Ton Hd INT.

x HEAT TREAT#_ R-12 FINAL DATE 5-25-68 TE:MPERA TURE Hour

- T'E-Minutes 500-600 I

2 30 600-700 1

50 700-800 1

37 800-900 5

50 900:.1000 35 1000-1100 1

50 1100-1175 35 1175-1200 1200-1100 1100-1000 25 1000-900 25 900-800 34 800-700 45 700-600 45 600-500 1

10 800-900 TOTAL 6 hours6.944444e-5 days 0.00167 hours 9.920635e-6 weeks 2.283e-6 months 24 min.

900-1000 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 1000-1100 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 15 min.

1100-1175 TOTAL 35 min.

1175-1200 TOTAL MAXIMl.Jl\\'1 TEMPERATURE 1205 DEGREES FARENHEIT t< Local heat treat a 1hes onl to the u er 5 feet of the u pp y

pp pp er shell.

Pg 8 of 10 45 min.

1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 6 hrs 30 min.

4 hrs 15 min.

40 min.

2 hrs 37 min.

25 min.

35 min.

30 min.

45 min.

50 min.

1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 7 hrs 15 min.

4 hrs 45 min.

1 hr 15 min.

2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 37 min.

- These temperature readings represent a single thermocouple at the 12:00 position of the furnace set-up. This T.C. was on the upper shell. This T.C. ran its own course approximately 200-250 degrees higher than the remaining thermocouples. The time inside the table does not include this "maverick" thennocoup le.

CONTRACT 2966 B-1 S.G.

Pg 9 of 10

Local Heat Treat C01\\'1PONE~1-Ugger Shell/To12 Head INT.

x HEAT TREAT# R-22 FINAL DATE 6-11-68 TEl\\ilPERA TURE Hour

-T'E-Minutes 500-600 410/680 Spread 2

600-700 5001715 Spread 2

700-800 620/800 Spread 23 800-900 720/860 Spread 52 900-1000 830/960 Spread 52 1000-1100 4

1100-1175 4

5 1175-1200 1100:.1000 22 1000-900 22 900-800 22 800-700 30 700-600 37 600-500 800-900 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 14 min.

900-1000 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 14 min.

1000-1100 TOTAL 4 hours4.62963e-5 days 0.00111 hours 6.613757e-6 weeks 1.522e-6 months 22 min.

1100-1175 TOTAL 4 hours4.62963e-5 days 0.00111 hours 6.613757e-6 weeks 1.522e-6 months 5 min.

\\-lAXThf.l; ~l TEl\\.'lPERA TURE 1140 DEGREES F ARENHEIT

Local heat treat would apply only to the top 5 feet of the upper shell assembly.

- Thermocouple temperature spread shown above was averaged to obtain nominal temperature.

CONTRACT 2966 B-1 S.G.

Pg 10 of 10 COMPO~"EN'l General Assembly INT.

HEAT TREAT# R-68 _

FINAL x DATE 8-30-68 TE:MPERA TURE Hour

- TIME-Minutes 500-600 12 600-700 5

700-800 -.

8 20 800-900 13 40 900-1000 9

20 1000-1100 10 1100-1175 13 1175-1200 1100-1000 3

40 1000-900 4

40 900-800 20 800-700 11 700-600 9

600-500 4

30 800-900 TOTAL 33 hours3.819444e-4 days 0.00917 hours 5.456349e-5 weeks 1.25565e-5 months 40 min.

900-1000 TOTAL 14 hours1.62037e-4 days 0.00389 hours 2.314815e-5 weeks 5.327e-6 months 1000-1100 TOTAL 13 hours1.50463e-4 days 0.00361 hours 2.149471e-5 weeks 4.9465e-6 months 40 min.

1100-1175 TOTAL 13 hours1.50463e-4 days 0.00361 hours 2.149471e-5 weeks 4.9465e-6 months

\\.lAXIML~I TEMPERATURE 1160 DEGREES F ARENHEIT

CONTRACT 2966 A-R. V.

Pg 1of11 COMPONENT Int. Shell INT.

x HEAT TREAT# N-17 FINAL DATE 11-12-66 TEMPERATURE Hour

- TIME-Minutes 500-600 50 600-700 25 700-800 30 800-900 30 900-1000 40 1000-1100 l

lO 1100-1175 30 1175-1200 1100-1000 55 1000-900 l

10 900-800 l

20 800-700 700-600 600-500 800-900 TOTAL l hour 50 min.

900-1000 TOTAL l hour 50 min.

1000-1100 TOTAL 2 hour2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 5 min.

1100-1175 TOTAL 30 min.

'lAXThIUM TEMPERATURE 1125 DEGREES FARENHEIT

CONTRACT 2966 A - R. V.

Pg 2 of 11 COMPONENT Int. Shell INT.

x HEAT TREAT# N FINAL DATE 2-24-67 TEMPERATURE Hour

- TIME-Minutes 500-600 50 600-700 50 700-800 40 800-900 1

10 900-1000 1

50 1000-1100 3

1100-1175 1

30 1175-1200 1100-1000 1

1000-900 1

30 900-800 1

50 800-700 1

30 700-600 2

20 600-500 2

10 800-900 TOTAL 3 hours3.472222e-5 days 8.333333e-4 hours 4.960317e-6 weeks 1.1415e-6 months 900-1000 TOTAL 3 hours3.472222e-5 days 8.333333e-4 hours 4.960317e-6 weeks 1.1415e-6 months 20 min.

1000-1100 TOTAL 4 hours4.62963e-5 days 0.00111 hours 6.613757e-6 weeks 1.522e-6 months 1100-1175 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 30 min.

\\lAXIMl.JM TEMPERATURE 1140 DEGREES FARENHEIT

CONTRACT 2966 A - R. V.

Pg 3 of 11 COI\\-IPONENT Lower Shell INT.

x HEAT TREAT# N FINAL DATE 2-4-67 TEIVIPERA TURE Hour

-T'E-Minutes 500-600 40 600-700 50 700-800 1

800-900 1

10 900-1000 40 1000-1100 -

1 10 1100-1175 20 1175-1200 1100-1000 1

1000-900 1

50 900-800 1

30 800-700 700-600 600-500 800-900 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 40 min.

900-1000 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 30 min.

1000-1100 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 10 min.

1100-1175 TOTAL 20 min.

MAXThUJM TEI\\-IPERA TURE 1125 DEGREES F ARENHEIT

CONTRACT 2966 A-R. V.

Pg 4 of 11 COMPONENT Lower Shell INT.

x HEAT TREAT # N-81 FINAL DATE 3-25-67 TEMPERATURE Hour

-TIME-Minutes 500-600 35 600-700 40 700-800 40 800-900 30 900-1000 50 1000-1100 1

50 1100-p75 20 1175-1200 1100-1000 50 1000-900 1

30 900-800 1

30 800-700 40 700-600 600-500.

800-900 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 900-1000 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 20 min.

1000-1100 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 40 min.

1100-1175 TOTAL 20 min.

MAXIl\\UJM TEMPERATURE 1140 DEGREES F ARENHEIT

CONTRACT 2966 A - R. V.

Pg 5 of 11 C01\\.'1PONENT Lower Shell INT.

x HEAT TREAT# 0-IZ FINAL DATE 5-22-67 TEMPERATURE Hour

- TIME-Minutes 500-600 50 600-700 40 700-800 50 800-900 50 900-1000 40 1000-1100 1

5 1100-1175 2

20 1175-1200 1100-1000 1

20 1000-900 1

30 900-800 2

800-700 1

700-600 1

20 600-500 800-900 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 50 min.

900-1000 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 10 min.

1000-1100 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 25 min.

1100-1175 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 20 min.

\\l~XIMUM TEMPERATURE 1125 DEGREES FARENHEIT

CONTRACT 2966 A - R. V.

Pg 6 of 11 COl\\tlPONENT Lower Shell INT.

x HEAT TREAT# 0-29 FINAL DATE 6-19-67 TEMPERATURE Hour

-T'E-Minutes 500-600 40 600-700 25 700-800 35 800-900 40 900-1000 40 1000-1100 1

30 1100-1175 30 1175-1200 1100-1000 50 1000-900 1

30 900-800 1

20 800-700 700-600 600-500 800-900 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 900-1000 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 10 min.

1000-1100 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 20 min.

1100-1175 TOTAL 30 min.

'.\\ilAXJl\\ilUM TEMPERATURE 1125 DEGREESFARENHEIT

CONTRACT 2966 A-R. V.

Pg 7 of 11 COMPONENT Bottom Hd/Lower Shell INT.

x HEAT TREAT# P-1 FINAL DATE 10-27-67 TEMPERATURE Hour

- TIME-Minutes 500-600 40 600-700 30 700-800 30 800-900 30 900-1000 1

1000-1100 40 1100-1175 20 1175-1200 1100-1000 40 1000-900 50 900-800 1

30 800-700 40 700-600 600-500 800-900 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 900-1000 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 50 min.

1000-1100 TOTAL 1 hour1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 20 min.

1100-1175 TOTAL 20 min.

.\\lAXThlL~l TEMPERATURE 1120 DEGREES F ARENHEIT

~

CONTRACT 2966 A-R. V.

Pg 8 of 11 COl\\tlPONENT Vessel ASsembly INT.

x HEAT TREAT # P-40 FINAL DATE 1-8-68 TEMPERATURE Hour

-TIME-Minutes 500-600 1

10 600-700 50 700-800 620/800 Spread 1

20 800-900 720/860 Spread 1

10 900-1000 830/960 Spread 2

1000-1100 1

40 1100-1175 20 1175-1200 1100-1000 1

1000-900 2

30 900-800 2

50_

800-700 1

10 700-600 600-500 800-900 TOTAL 4 hours4.62963e-5 days 0.00111 hours 6.613757e-6 weeks 1.522e-6 months 900-1000 TOTAL 4 hours4.62963e-5 days 0.00111 hours 6.613757e-6 weeks 1.522e-6 months 30 min.

1000-1100 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 40 min.

1100-1175 TOTAL 20 min.

MA.'XL\\UJl\\tl TEMPERATURE 1120 DEGREES FARENHEIT

CONTRACT 2966 A - R. V.

Pg 9 of 11 COMPONENT Vessel Assembly INT.

x HEAT TREAT# P-71 FINAL DATE 3-11-68 TEMPERATURE Hour

- TIME-Minutes 500-600 1

600-700 1

10 700-800 1

30 800-900 1

30 900-1000 1

20 1000-1100 1

10 1100-1175 20 1175-1200 1100-1000 1

1000-900 2

10 900-800 3

10 800-700 2

700-600 600-500 800-900 TOTAL 4 hours4.62963e-5 days 0.00111 hours 6.613757e-6 weeks 1.522e-6 months 40 min.

900-1000 TOTAL 3 hours3.472222e-5 days 8.333333e-4 hours 4.960317e-6 weeks 1.1415e-6 months 30 min.

1000-1100 TOTAL 2 hours2.314815e-5 days 5.555556e-4 hours 3.306878e-6 weeks 7.61e-7 months 10 min.

1100-1175 TOTAL 20 min.

\\IAXIl\\U.TM TEMPERATURE 1120 DEGREES FARENHEIT

CONTRACT 2966 A - R. V.

Pg 10 of 11 COMPONENT Vessel Assembly INT.

x HEAT TREAT # P-94 FINAL DATE 4-23-68 TEMPERATURE Hour

- TIME-Minutes 500-600 50 600-700 50 700-800 50 800-900 40 900-1000 1

20 1000-1100 1

5 1100-1175 20 1175-1200 1100-1000 40 1000-900 1

40 900-800 2

30 800-700 700-600 600-500 800-900 TOTAL 3 hours3.472222e-5 days 8.333333e-4 hours 4.960317e-6 weeks 1.1415e-6 months 10 min.

900-1000 TOTAL 3 hours3.472222e-5 days 8.333333e-4 hours 4.960317e-6 weeks 1.1415e-6 months 1000-1100 TOTAL 1 hours1.157407e-5 days 2.777778e-4 hours 1.653439e-6 weeks 3.805e-7 months 45 min.

1100-1175 TOTAL 20 min.

.\\lA,XL'HUM TEMPERATURE 1120 DEGREES FARENHEIT

CONTRACT 2966 A - R. V.

Pg 11of11 COMPONENT Vessel Assembly INT.

HEAT TREAT# R-7 FINAL x DATE 5-17-68 TEMPERATURE Hour

-T'E-

.Minutes 500-600 2

30 600-700 2

30 700-800 2

20 800-900 2

900-1000 1

30 1000-1100 2

20 1100-1175 13 15 1175-1200 1100-1000 2

20 1000-900 2

50 900-800 3

40 800-700 3

50 700-600 5

40 600-500 800-900 TOTAL 5 hours5.787037e-5 days 0.00139 hours 8.267196e-6 weeks 1.9025e-6 months 40 min.

900-1000 TOTAL 4 hours4.62963e-5 days 0.00111 hours 6.613757e-6 weeks 1.522e-6 months 20 min.

1000-1100 TOTAL 4 hours4.62963e-5 days 0.00111 hours 6.613757e-6 weeks 1.522e-6 months 40 min.

1100-1175 TOTAL 13 hours1.50463e-4 days 0.00361 hours 2.149471e-5 weeks 4.9465e-6 months 15 min.

\\IA.. X~ll.TM TEMPERATURE 1165 DEGREES FARENHEIT

Effect of Chemical Composition & Thermal History on RPV & SG Weld Metal Properties INTRODUCTION A decrease in the toughness properties of low alloy pressure vessel steels and their weld metals can occur when certain materials are slowly cooled or held at temperatures in the range of 700°F to 1100°F.

The changes in toughness properties are commonly refered to as temper embrittlement, since exposure to this temperature range is generally associated with tempering of the steel or postweld heat treatment of weldments. This form of embrittlement is also commonly referred to as 885°F embrittlement because certain materials, such as martensitic stainless steels, exhibit a maximum degree of embrittlement after exposure at this temperature. The temperature range of 800°F to 1000°F is generally considered to be the most significant for temper embrittlement for the low alloy steels typically used in the fabrication of reactor pressure vessel and steam generator components. Temper embrittlement results in a shift of the transition in Charpy V-Notch energy curves to higher temperatures. Upper shelf energy (USE) is generally reported to be unaffected by temper embrittlement.

However, in contradiction to this observation some materials are reported to have reduced USE values after thermal aging. Brittle fracture mode in the lower shelf region becomes intergranular following prior austenite grain boundaries in temper embrittled material. A larger prior austenite grain size increases the degree of embrittlement and intergranular fracture.

Base metal and weld metal properties can be influenced by temper embrittlement effects.

Weld metals may be more susceptible to such effects than base metals.

The two major factors affecting susceptibility and degree of temper embrittlement are the alloy chemical composition and thermal history of the material. Key variables related to these factors are discussed below.

COMPOSITION EFFECTS Temper embrittlement can occur in various alloy steels when impurities, such as phosphorus (P),

tin (Sn), antimony (Sb) and arsenic (As) segregate at grain boundaries during exposure at temperatures in the range of 700°F to 1100°F. Increased concentrations of these impurities generally results in decreased fracture toughness and a susceptibility to further degradation of toughness due to continued aging during service. Manganese (Mn) and silicon (Si) can also have an embrittling effect when present in large quantities. The temper embrittlement mechanism is generally not significant for the low alloy pressure vessel steels used in nuclear components because of material composition and controls used in manufacture.

The role of copper in the temper embrittlement mechanism is not clear. Hasegawa (1) concluded that 0.37% copper in SA533B plate contributed to temper embrittlement after aging at temperatures between 570°F and 1110°F.

Transition temperature shifts were observed after aging for times of 100 and 1000 hours0.0116 days 0.278 hours 0.00165 weeks 3.805e-4 months . The commercial compositions of SA533B exhibited

shifts of about 50°F. The copper doped alloy exhibited the largest shifts after aging at 930°F of approximately 200°F after 100 hours0.00116 days 0.0278 hours 1.653439e-4 weeks 3.805e-5 months and 290°F after 1000 hours0.0116 days 0.278 hours 0.00165 weeks 3.805e-4 months .

The high copper plate exhibited larger shifts after aging than either a commercial grade composition or a phosphorus doped heat of material. Druce and Edwards (2) did not observe a strong influence of 0.4%

copper in another heat of SA533B plate. Aging in the temperature range of 570°F to i 110°F for times from 100 to 5000 hours0.0579 days 1.389 hours 0.00827 weeks 0.0019 months produced varying degrees of embrittlement. Aging of the O.4 %

copper doped alloy, with a large prior austenite grain size, exhibited transition temperature shift and USE drop after aging for 1000 hours0.0116 days 0.278 hours 0.00165 weeks 3.805e-4 months at 930°F. However, the 0.045% phosphorus doped alloy exhibited a greater degree of embrittlement after the same aging treatment. An interaction of phosphorus and copper was suggested because Auger analysis of intergranular fracture surfaces detected the presence of both phosphorus and copper on the grain boundary surfaces.

The Cu, P, Sn, and As contents of the Palisades SG weld samples as determined by Optical Emission Spectroscopy (OBS) are shown in Tables l and 2. Antimony (Sb) was not reported from any of the chemical analyses performed on these samples. The reported levels of P, Sn and As would not be expected to produce a significant effect on toughness due to temper embrittlement.

There is essentially no difference in the impurity elements associated with temper embrittlement effects for these two heats of weld wire. There is only a relatively small difference in the copper values reported for the two heats (0.29% average for W5214 vs. 0.19%

average for 34B009). Based on these reported weld chemistries for the two heats of wire no significant differences in thermal aging response would be expected.

THERMAL IDSTORY EFFECTS Thermal history of low alloy steels is a major factor in determining the temper embrittlement effects on toughness properties. Thermal exposures during component fabrication and operation may contribute to changes in toughness properties of a susceptible material. If a material is susceptible, temper embrittlement will occur when the material is either slow cooled or held in the temperature range of 700°F to 1100°F.

The effects of temper embrittlement can be minimized by rapid cooling of susceptible material through the_embrittling temperature range.

Temper embrittlement effects are usually reversible.

By re-heating the temper embrittled material to the tempering temperature and assuring rapid cooling through the embrittling range, the toughness properties of the material can be restored.

Studies have shown that slow cooling or step cooling of steels containing impurity elements discussed above results in increases* in ductile-to-brittle transition temperatures. Step cooling of an SA533B and SA302C plate materials resulted in 10°F to 55°F increases in the 40 ft-lb transition temperature (3). The upper shelf energies (USE) for the step cooled material exhibited between 0 and 10 % decreases for the same materials.

SA302B submerged arc weld metal exhibited a 50°F shift in transition temperature after step cooling with a 19% decrease in USE.

Evaluation of submerged arc weld metals exposed to slow cooling or step-cooling revealed increased transition temperatures due to temper embrittlement. Extended times up to 90 hours0.00104 days 0.025 hours 1.488095e-4 weeks 3.4245e-5 months at 900-950°F following postweld heat treatment at 1100-1150°F resulted in the largest decrease in Charpy impact properties.

Comparable effects were achieved with very slow ( < 10°F/Hr.)

coolmg rates from 1100°F.

The embrittlement was reversible by reheating to the PWHT

temperature range followed by more rapid cooling. There was also a significant heat-to-heat variability in the response of the weld material to the various thermal histories. Some heats showed only minimal degradation while other heats exhibited relatively large increases in transition temperatures.

The cooling times and rates from the final PWHT for the Palisades steam generators and reactor vessel are shown in Table 3. The reactor vessel cooling rate was significantly faster than either of the steam generators. This fact suggests that if there is a potential thermal aging effect for the weld metals, the effects would be minimized in the reactor vessel welds due to the faster cooling rate.

The cooling rates for both steam generators were generally slow with no remarkable differences. Steam generator assembly #1 had a very slow average cooling rate from 900°F to 850°F. However, steam generator assembly #2 had a similar slow cooling rate from 950°F to 900°F. The overall cooling time duration in the range 1000-800°F was comparable for both steam generator assemblies. There is no obvious difference between the two thermal histories that can be used to rationalize the differences in Charpy impact properties. Additional Charpy impact testing, microstructural evaluation and fractographic examination of fracture surfaces from the materials following simulated PWHT thermal histories may provide an explanation for the weld metal toughness properties.

The effect of operating exposure on thermal aging of weld and base materials of RPV' s has been evaluated by means of thermal surveillance capsules. These capsules were inserted in RPV or other locations for exposure to the plant operating temperatures.

Evaluations of operating service thermal exposure generally indicate that thermal aging is not a significant degradation mechanism for NSSS components because of the material selection and relatively low operating temperatures relative to the range where temper embrittlement effects have been observed.

Results of the Palisades thermal capsule reported shifts of 60-70°F for the weld and HAZ material due to thermal exposure at 535°F. However, there was considerable scatter in the CVN test data for the weld and HAZ materials which makes interpretation of results difficult. An independent analysis of the same CVN data resulted in a calculated shift of only 30°F. Similar thermal capsule results were reported on weld metal specimens aged at 550°F for 63,000 hours0 days 0 hours 0 weeks 0 months at the Doe! plant. A 30 ft-lb. shift of approximately 54°F was reported for the weld metal. This data set also exhibited a large degree of scatter~ Other thermal capsules have reported little or no effect of operating temperature thermal exposure on surveillance materials, including several high copper weld metals (0.27-0.32 % Cu). Both Palisades steam generators experienced the same service history at temperatures in the range of 500°F for approximately 90,345 hours0.00399 days 0.0958 hours 5.704365e-4 weeks 1.312725e-4 months . The W5214 weld metal exhibited some variation in properties compared to previous test results, while the 34B009 weld metal test results were very similar to earlier data. Although the trend curves are similar, there is considerable scatter in the combined 34B009 data set. Because of the low service temperature and the inconsistent response of the materials, it is unlikely that the operating thermal exposure would cause a significant change in toughness properties.

SUMMARY

& CONCLUSIONS Studies have shown that extended times at temperatures below the PWHT range or slow cooling following PWHT can affect the impact toughness properties of RPV base and weld metals. Test

results exhibit a significant heat-to-heat variability, some heats showing minimal degradation while other heats of similar material show increased susceptibility to thermal aging effects.

The low alloy steels and weld metals used to fabricate the Palisades reactor pressure vessel (RPV) have relatively low susceptibility to thermal aging effects. Furthermore, rapid cooling following the final PWHT minimized the potential for temper embrittlement.

The Palisades steam generator was subjected to a significantly longer time in the temper embrittlement temperature range than the RPV during the final PWHT. The time was long enough to have caused some temper embrittlement, but the extent can not be quantified based on published information.

No clear explanation of the differences in Charpy impact properties between the Palisades steam generator welds can be provided based on chemical composition or thermal history effects.

Additional testing of Charpy impact specimens from material exposed to different PWHT thermal histories may provide a rationale for the differences in test data.

Microstructural and fractographic evaluation of the material and test specimen fracture surfaces may also provide s~me evidence to explain the variation in properties.

Removal of the apparent temper embrittlement could be accomplished by an additional PWHT at 1125°F (contingent on the results of additional metallurgical evaluation).

REFERENCES

1)

2)

3)

M. Hasegawa, et al., Trans. JIM, Vol. 16, 1975, pp. 641-646.

S. G. Druce and B. C. Edwards, Nuc. Tech., Vol. 55, 1981, pp. 487-498.

R. A. Swift and J. A. Guyla, Welding Research Supplement, February 1973, pp 57s-68s.

TABLE 1 IMPURITY CONTENT OF PALISADES SG A - W5214 WELD SAMPLES SAMPLE

%Cu 3P

%Sn

%As Al/1-X 0.'.33 0.011 0.008 0.009 Al/1-Y 0.30 0.013 0.008 0.010 Al/1-Z 0.25 0.012 0.007 0.009 A/SG/A/2-X 0.37 0.011 0.008 0.010 A/SG/A/2-Y 0.29 0.013 0.008 0.010 A/SG/A/2-Z 0.27 0.013 0.008 0.010 A/SG/B/3-X 0.34 0.011 0.008 0.010 A/SG/B/3-Y 0.22 0.012 0.008 0.010 A/SG/B/3-Z 0.22 0.011 0.008 0.010

*-~---

TABLE 2 Th1PURITY CONTENT OF PALISADES SG B - 34B009 WELD SAMPLES SAMPLE

%Cu

%P

%Sn

%As Bl/2-X 0.21 0.014 0.007 0.011 Bl/2-Y 0.18 0.013 0.006 0.010 Bl/2-Z 0.19 0.014 0.007 0.012 B/SG/N2-X 0.18 0.014 0.008 0.012 BISG/N2-Y 0.18 0.013 0.007 0.010 B/SG/A/2-Z 0.19 0.013 0.007 0.011 B/SG/B/2-X 0.15 0.013 0.007 0.011 B/SG/B/2-Y 0.20 0.013 0.007 0.012 B/SG/B/2-Z 0.20 0.013 0.007 0.011

TABLE 3 FINAL PWHT COOLING TIMES AND RATES FOR PALISADES COMPONENTS COMPONENT TEMPERATURE COOLING TIM~

COOLING RA TE RANGE (°F)

(Hrs.)

(°F/Hr.)

STEAM GENERATOR 1000-950 2

25 ASSEMBLY 1 950-900 2.67 18.7 900-850 13.67 3.6 850-800 6.33 7.9 24.67 TOTAL 8.1 AVG.

STEAM GENERATOR 1000-950 6.33 7.9 ASSEMBLY2 950-900 8.67 5.7 900-850 6.67 7.5 850-800 5.33 9.4 27.00TOTAL 7.4 AVG.

REACTOR PRESSURE 1000-950 1.42 35.2 VESSEL 950-900 1.42 35.2 900-850 2.1 23.8 850-800 1.58 31.6 6.52 TOTAL 30.7 AVG.

ATTACHMENT NO. 2 Consumers Power Company Palisades Plant Docket 50-255 RESPONSE TO NRC NOVEMBER 30,1994 REQUEST FOR ADDITIONAL INFORMATION REVISION 1 10CFR50.61 SCREENING CRITERION ITEM NO. 2 ABB CENO RESPONSE There are no changes from Revision 0.

2 Pages

ABB - CENO RESPONSE The Charpy and drop weight data from the steam generator weld samples have been compared to the generic weld data base.

Available data that demonstrate typical variability of the drop weight nil-ductility transition temperarure (NDTT) and the unirradiated reference temperature (RT NOT) for a specific heat of weld wire are shown in Table 1. When there are two test results for a single wire heat the NDTT and RTNoT temperarures are found to vary 10

F to 30

F b_etween the results.

The value of RTNDT is determined by the minimum of the NDTT or Tcv-60' F, where Tcv is the Charpy test temperature at which 50 ft-lbs. absorbed energy and 35 mils lateral expansion are achieved. In some cases the NDTT result controls the RT NOT value and NDIT equals RTNoT* In other cases, Tcv-60 is the limiting value for RTNDT and RT1>mT will be higher than the NDTT value. In many cases the actual Tcv is not determined.

Charpy impact tests are performed at NDTT+60"F and if the 50 ft-lb and 35 mil criteria are satisfied no further testing is required.

In some cases, the Charpy results at NDIT+60"F could be as much as 90 to 100 ft-lb or the test result could just meet the minimum 50 ft-lb requirement.

In'. such cases, the RTNoT values can be the same or similar because it is controlled by NDTT but the Charpy impact properties for two welds with the same NDTT can be dramatically different. From Table 1, RT NOT varies by lO'F to 30"F when the RTNoT is controlled by NDTT.

In other cases, the Charpy test results at NDTT+60"F may not meet the 50 ft-lb. and 35 mils requirements. When this happens testing is performed at higher temperatures until the criteria are met.

This higher temperature then becomes T cv and T cv-60

F determines the RTNoT* This can be seen in Table 1 for wire heats 13253 and 3P8013 where the RT :-mT values are higher than the corresponding NDTT value. The RT :-;or varies by 10' F when the Charpy impact properties are limiting.

The P:ilisades steam generator A, Weld 1-951 Charpy and drop-weight test data produced an RT 'iDT of -20

F for weld wire heat W5214. This was controlled by drop-weight test results for NDTT. The NDTT could have been -30' F, if specimens 9 and 10 happened to be tested before specimen number 5 which broke at -20'F. The results on W521~

reflect some of the inherent variability in the drop-weight test method. Another factor introducing variability is the comparison of the W5214 test results using single pass weld bead deposits and comparing to earlier data performed on specimens with two pass weld bead deposits. Examination of the Charpy impact data from the W5214 shows the 50 ft-lb Tcv to be approximately 20"F. This is determined from the minimum data points from the full Charpy impact curve in accordance with NB-2331(4). This Tcv would

I I

support an RT ~oT value as low as -40

F.

In sununary, the data from the SG weld are consistent with the data set from the generic database on similar welds. The measured RT!'mT value is within the observed range of variation for -these types of weld materials.

However, sufficient uncertainty exists relative to the condition of the SG weld material for it to be considered as being specifically representative of the initial baseline properties of the RV weld seams. The evaluation of RAI #3 for Charpy energy properties suggests statistically significant differences between the SG weld and other baseline properties from W5214 welds.

Therefore, it is appropriate to continue using the generic mean value of -56°F for the RV W5214 welds.

TABLE 2-1 v ARIABILITY IN NDTT AND RTNDT I

HEAT OF WIRE I FLUX TYPE I

NDTT l

RT!'IDT I

13253 1092

-40

-70

-50 83650 0091

-10

-40

-40 l

I 3P8013 124

-60

-50

-80

-60 88114 0091

-70

-80

-80 89833 0091

-50

-60

-60 90069 0091

-60

-60 I

-70

-70 33.A.277 0091

-60

-80

-80 I

IP3571 1092

-30

-50

ATTACHMENT NO. 2A Consumers Power Company Palisades Plant Docket 50-255 RESPONSE TO NRC NOVEMBER 30,1994 REQUEST FOR ADDITIONAL INFORMATION REVISION 1 10CFR50.61 SCREENING CRITERION ITEM NO. 2 ATI CONSULTING RESPONSE Ther are no changes from Revision O.

10 Pages

VARIABILITY OF DROP-WEIGHT NDT DATA FOR HEATS OF C-E FABRICATED WELDS Compiled by T. J. Griesbac~ ATI Consulting Here are the results of my initial survey of drop-weight NDT data for multiple measurements on single heats ofC-E fabricated welds in support of Item 2:

lieatNo.

Flux Type DWNPTT(0F)

Sources*

1P3571 Linde 1092

-30, -50 MY, WPS Surv.

13253 Linde 1092

-40, -70 SA2, CKl Surv.

33A277 Linde 0091

-60, -80 FAl, CCI Surv.

90069 Linde 0091

-60, -70 C-E WQTests It is observed that the variation in measured drop-weight data is on the order of 10 to 3 0°F within a single heat of material.

This data was gathered from the A TI Consulting RPVDATA database. Printouts containg the data and source reference information are attached.

TJG December 9, 1994

Weld Qualification and Test Data for Heat No. 1P3571 Measured Test Results of Chemistry and Mechanical Properties of Welds WIRE HEAT NO: 1P3571 WIRE TYPE: B-4 MOD FLUX TYPE: LINDE 1092 SOURCE: MY,SC Ni WIRE:

WIRE DIA: 3/16 in.

FLUX LOT: 3958 QUAL CODE:

Cu:

0.36 Ni:

0.78 C:

0.14 Mn:

1.38 P:

0.015 S:

0.012 Si:

Mo:

0.55 Cr:

0.07 DWNDTT:

-30 deg F RTNDT:

-30 deg F IUSE:

107 ft-lbs YS:

62.6 ksi UTS:

85.2 ksi ELONG. IN l":

24.2 %

REDUCTION IN AREA:

59.3 %

REFERENCE:

CR-75-269 TEST DATE:

LAB SAMPLE NO:

RPVDA TA developed by ATI Consulting

Weld Qualification and Test Data for Heat No. 1P3571 Measured Test Results of Chemistry and Mechanical Properties of Welds WIRE HEAT NO: 1P3571 WIRE TYPE: B-4 Mod FLUX TYPE: Linde 1092 NIWIRE:

WIRE DIA: 3/16 in.

FLUX LOT: 3958 Cu:

NI:

C:

P:

S:

Si:

Cr:

DWNDTT:

-50 deg F RTNDT:

degF IUSE:

SOURCE: WPS Test Data QUALCODE: NIA Mn:

Mo:

ft-lbs YS:

ksi UTS:

ksi ELONG. IN 2":

REDUCTION IN AREA:

REFERENCE:

TEST DATE:

9/1/94 LAB SAMPLE NO:

RPVDAT A developed by ATI Consulting

Weld Qualification and Test Data for Heat No. 13253 Measured Test Results of Chemistry and Mechanical Properties of Welds WIRE HEAT NO : 13253 WIRE TYPE: B-4 MOD FLUX TYPE: LINDE 1092 SOURCE: SA2,SC Ni WIRE:

WIRE DIA: 3/16 in.

FLUX LOT: 3774 QUAL CODE:

Cu:

0.23 Ni:

0.71 C:

0.1 Mo:

1.27 P:

0.017 S:

0.011 Si:

Mo:

0.45 Cr:

0.015 DWNDTT:

-40 deg F RTNDT:

-40 deg F IUSE:

111 ft-lbs YS:

57.7 ksi UTS:

78.6 ksi ELONG. IN l":

20.3 %

REDUCTION IN AREA:

60.5 %

REFERENCE:

WCAP-8824 TEST DATE:

LAB SAMPLE NO:

RPVDAT A developed by ATI Consulting

Weld Qualification and Test Data for Heat No. 13253 Measured Test Results of Chemistry and Mechanical Properties of Welds WIRE HEAT NO: 13253 WIRE TYPE: B-4 MOD FLUX TYPE: LINDE 1092 SOURCE: CKl,SC NIWIRE:

WIRE DIA: 3/16 in.

FLUX LOT: 3791 QUAL CODE:

Cu:

0.27 NI:

0.74 C:

0.26 Mo:

1.33 P:

0.023 S:

0.014 Si:

Mo:

0.44 Cr:

0.022 DWNDTT:

-70 deg F RTNDT:

-70 deg F IUSE:

110 ft-lbs YS:

56.8 ksi UTS:

79 ksi ELONG. IN 2":

23.5 %

REDUCTION IN AREA:

64.3 %

REFERENCE:

WCAP-8047 TEST DATE:

LAB SAMPLE NO:

RPVDA TA developed by ATI Consulting

Weld Qualification and Test Data for Heat No. 33A277 Measured Test Results of Chemistry and Mechanical Properties of Welds WIRE HEAT NO: 33A277 WIRE TYPE: B-4 FLUX TYPE: LINDE 0091 SOURCE: FAI,SC Ni WIRE:

WIRE DIA: 3/16 in..

FLUX LOT: 3922 QUAL CODE:

Cu:

0.14 Ni:

0.19 C:

0.13 Mn:

1.06 P:

0.016 S:

0.009 Si:

Mo:

0.5 Cr:

0.063 DWNDTI:

-60 deg F IRTNDT:

-60 deg F IUSE:

149 ft-lbs YS:

68.2 ksi UTS:

87.2 ksi ELONG. IN 2":

20.6 %

REDUCTION IN AREA:

65.8 %

REFERENCE:

WCAP-8810 TEST DATE:

LAB SAMPLE NO:

RPVDAT A. developed by ATI Consulting 23

Weld Qualification and Test Data for Heat No. 33A277 Measured Test Results of Chemistry and Mechanical Properties of Welds WIRE HEAT NO : 33A277 WIRE TYPE: B-4 FLUX TYPE: LINDE 0091 SOURCE: CCl,SC NlWIRE:

WIRE DIA: 3/16 in.

FLUX LOT: 3922 QUAL CODE:

Cu:

0.24 Ni:

0.18 C:

0.15 Mn:

1.05 P:

0.014 S:

0.013 Si:

Mo:

0.55 Cr:

0.06 DWNDTI:

-80 deg F IRTNDT:

-80 deg F IUSE:

160 ft-lbs YS:

72.1 ksi UTS:

85.1 ksi ELONG. IN 2":

26.8%

REDUCTION IN AREA:

71.8%

REFERENCE:

TR-ESS-001 TEST DATE:

LAB SAMPLE NO:

RPVDA TA developed by A TI Consulting 25

Weld Qualification and Test Data for Heat No. 90069 Measured Tes/ Results of Chemistry and Mechanical Properties of Welds WIRE HEAT NO : 90069 WIRE TYPE: LCLP FLUX TYPE: LINDE 0091 SOURCE: CE,WQ Ni WIRE:

WIRE DIA: 3/16 in.

FLUX LOT: 1054 QUAL CODE: 03.19 Cu:

0.05 Ni:

0.03 C:

0.14 Mo:

1.26 P:

0.006 S:

0.006 Si:

0.16 Mo:

. 0.51 Cr:

0.04 DWNDTT:

-70 deg F IRTNDT:

-70 deg F IUSE:

156 ft-lbs YS:

77.2 ksi UTS:

89.9 ksi ELONG. IN 2":

27%

REDUCTION IN AREA:.

70 %

REFERENCE:

C-E 78-12 RSP TEST DATE:

4/2/76 LAB SAMPLE NO: 023726 RPVDA TA developed by A Tl Consulting 5

Weld Qualification and Test Data for Heat No. 90069 Measured Test Results of Chemistry and Mechanical Properties of Welds WIRE HEAT NO : 90069 WIRE TYPE: B-4 FLUX TYPE: LINDE 0091 SOURCE: CE,WQ NIWIRE:

WIRE DIA: 3/16 in.

FLUX LOT: 0842 QUAL CODE: G2.05 Cu:

0.04 Ni:

0.04 C:

0.15 Mn:

1.12 P:

0.007 S:

0.008 Si:

0.19

. Mo:

0.49 Cr:

0.02 DWNDTT:

-60 deg F IRTNDT:

-60 deg F IUSE:

162 ft-lbs YS:

70 ksi UTS:

81.8 ksi ELONG. IN 2":

30.5 %

REDUCTION JN AREA:

74.9 %

REFERENCE:

C-E 78-12 RSP TEST DATE:

4/4175 LAB SAMPLE NO: DI ~893 RPVDATA developed by ATI Consulting 3

ATTACHMENT N0.3 Consumers Power Company Pali sades Pl ant Docket 50-255 RESPONSE TO NRC NOVEMBER 30,1994 REQUEST FOR ADDITIONAL INFORMATION REVISION 1 10CFR50.61 SCREENING CRITERION ITEM NO. 3 HYPERBOLIC TANGENT CURVE FITS AND ASSOCIATED STATISTICS BY ATI CONSUL TING

INTRODUCTION HYPERBOLIC TANGENT CURVE FITS AND ASSOCIATED STATISTICS by ATI Consulting W. L. Server B. F. Beaudoin B. N. Burgos The general shape of fracture toughness as a function of test temperature for ferritic steels is that of an 11S 11,generally with definable lower and upper shelves and a connecting region between the shelves called the transition region. Toughness data that can be modeled in this form are represented by the Charpy V-notch (or other notched geometry) fracture parameters or actual fracture toughness test results (using fatigue precracked test specimens) as a function of test temperature.

At temperatures on the lower shelf, ferritic steels are brittle generally showing a cleavage-type of fracture surface indicative of low toughness, while at higher temperatures on the upper shelf, the fracture surface indicates a much more ductile shear-type of fracture tearing which requires significantly greater fracture energy. The transition temperature region is a mixture of these two fracture types.

In the nuclear power industry, the basis for safe design and operation of the reactor pressure vessel and other ferritic steel pressure boundary components is predominantly impact Charpy V-notch test results. The key results are the fracture impact energy (CVN),

lateral expansion (LE), and fracture appearance (percent shear, %S). Other direct measurements of fracture. toughness are sometimes obtained and can be treated in a similar manner as Charpy V-notch data. Other factors, such as a sloping upper shelf, can complicate this simple analogy requiring some modification of the interpretation of the results.

The hyperbolic tangent (tanh) function has been used for some time as a statistical curve-fit tool to describe this "S 11-shaped response. Other functional relationships could have been used to produce a similar shape (eg., an error function), but the value of the tanh function is that the curve fit parameters defining the 11 S" shape have physical meaning relative to the response being evaluated from the test results:

Y = A + B tanh [(T - T0 ) I C]

(1) where (looking at Figure 1):

1

Y is the toughness response measurement (CVN, LE, %S, or fracture toughness) at a given temperature, T (A - B) is the asymptotic lower shelf level (A + B) is the asymptotic upper shelf level T0 is the mid transition temperature corresponding to A C is a measure of the slope of the transition regime (B/C is the actual slope at the temperature T 0 )

When the experimental toughness data display this general shape, the tanh curve-fit is an excellent engineering method for representing the measured data and for making comparisons SlJch as the response of neutron irradiation for pressure vessel steels as shown in Figure 2. The Charpy V-notch key measures of neutron irradiation are: the shift in temperature at the 30 ft-lb (41 J) and 50 ft-lb (68 J) energy levels (~T30 and ~T50,

respectively), the transition temperature shift at 35 mils (0.89 mm) lateral expansion

(~T35LiJ, and the drop in upper shelf energy (~USE). The change in transition temperature from the fracture appearance data at 50% shear (~T50%) can also be used as a measure of irradiation change. The most commonly used measure is the Charpy energy (CVN) since testing of Charpy specimens is generally the key element in reactor pressure vessel surveillance programs.

The purpose of this report is to describe the results of hyperbolic tangent curve-fits to CVN data representative of or similar to the limiting weld material (weld wire heat W5214) in the Palisades reactor pressure vessel. These curve-fit results are also evaluated statistically

. to determine the spread in the results for the key parameters derived from the tanh curves.

STATISTICAL INTERPRETATION The curve-fitting of the toughness data in the tanh model is relatively simple using the computers and numerical methods available today. However, the interpretation of the statistical parameters (assumed to be Gaussian or Normal) is more complicated because often some of the curve-fitting options are restricted and some statistical intervals in the temperature (T) direction must be assessed rather than in the Y direction (i.e., the asymptotic nature of the tanh relationship proves difficult when inverted and statistics are applied for temperature).

Of course, approximations can be made to assess the temperature intervals by plotting the Y intervals and determining graphically the spread in temperature, but this approach is somewhat cumbersome and only an estimation. It should be understood that making any statistical assessments at different levels of toughness other than at the mean model values of T0 and A are also only approximations.

2

One of the limitations of the tanh model is the ability to adequately fit results when there are no data on the lower and/or upper shelves. When little or no lower shelf data exist, the curve fit can either give an (A-B) value less than zero or a plateau at a level above zero that has no meaning. If CVN data were present at very low temperatures for ferritic pressure vessel steels, a lower shelf value of 1-2 ft-lbs would most likely be measured. For most applications, a fixed CVN lower shelf of about 2.2 ft-lb is a good approximation that gives the tanh model physical significance. Similarly, a fixed lower shelf of 1 mil LE and 0% shear are also appropriate values; for fracture toughness, a lower bound of around 25 -

30 ksi-in 112 is reasonable for most ferritic steels. When the lower shelf is fixed, the statistical significance of the curve fit is muddled in the region of the lower shelf and the degree of freedom is larger by one for the non-lower shelf region since *one of the curve fit parameters is eliminated.

In some cases where limited upper shelf data are measured, it may be appropriate to fix the upper shelf (often in addition to the lower shelf). Even when an upper shelf CVN level is achievable through curve fitting, it is often desirable to apply some specified method for defining the upper shelf. For instance, the ASTM El85-94 definition for upper shelf utilizing the 2:.. 95 % shear fracture appearance is an appropriate method for defining (fixing) the upper shelf. When the lower shelf is also fixed, the tanh fit relates only to the transition temperature regime. As in fixing the lower shelf, the upper shelf statistics are compromised in order to make the model achieve physical significance as determined by the engineer. A separate statistical argument can be made for the upper shelf using a subset of the entire data set (i.e., that portion of the data that is applicable to the upper shelf).

The use of the tanh model to data does not imply that the model is the only representation for the specific nature of the material since the specific fit can be influenced by the number and temperature location of the toughness data measurements.

Additionally, the data may suggest a more complex curve shape than the simple tanh "S"relationship; i.e., the upper shelf can have a slope with temperature either positive or negative or there can sometimes exist intermediate shelves when enough data are available to define them. For RPV steels, the tanh model generally describes the Charpy data, and with good engineering judgement, the user can tailor the tanh fit to optiffiize physical significance and still adequately fit the data from a statistical standpoint.

It is generally most appropriate to treat the data in-the transition temperature region separately from the upper shelf data for statistical evaluations, but the overall tanh fit should use all of the measured data unless specific data points can be justifiably removed.

Decisions on whether to fix shelves requires experience and engineering judgement. Our experience in fitting thousands of curves suggests that the lower shelf should generally be fixed as a constant for all comparisons; as indicated earlier, a value of 2.2 ft-lb for CVN data is reasonable.

The fixing of the upper shelf is dictated by the specific data values; in most cases where there are more than two or three upper shelf measurements (often at different test temperatures), whether the shelf is set free to be determined by the tanh least-squares regression or whether it is defined using the ASTM definition is generally 3

inconsequential since both will produce similar upper shelf energy results. However, there are cases where engineering judgement will suggest that it is appropriate to fix the upper shelf.

Statistically, the ta¢i regression analysis produces information that can be used to provide estimates of the variances and standard deviations for the individual fracture parameters.

The variance values can be derived from the overall fit or from subsets of the data in certain ranges. We feel that several different measures should be determined and compared for consistency, and the final choice of the interval or bound should be based upon an engineering evaluation of the different results. The following discussion describes a methodology which is applied to the weld wire W5214 data sets to evaluate the key fracture parameters and estimate their statistical spread (intervals).

The starting point is the tanh regression to the measured Charpy energy data ( CVN).

After applying engineering judgement relative to fixing the lower and upper shelves, the tanh curve regression can be performed to determine the least squares fit defining the values of A, B, T0, and C. From. this fit, the specific values of upper shelf energy (A+B) and transition temperature (T30 and T50) can be determined.

Additionally, the range of data in the transition region can be defined as (T 0 + C). From the least squares regression, the overall variance can be determined and the standard deviation at the specific model mean values of A and T0 can be calculated. Individual variances and covariances of the curve fit parameters can also be determined and used to determine confidence or prediction intervals at other points around the curve. Unfortunately, many of the measures that are used revolve about the temperature associated with a CVN value ( eg., T 30). The upper shelf energy value and intervals can be deduced directly based upon the entire curve fit, although as will be described later, the separation and use of only the data above (T0 +

C) can make good engineering sense.

In the transition region (T0 + C), three different approaches are suggested to estimate the confidence and prediction intervals: (1) a linear least squares fit to the inverted data in this temperature region (i.e., treating temperature as the dependent variable), (2) a forced linear fit in inverted space using the model mean value (T0, A) and slope C/B, and (3) an

. inverted tanh curve based upon the overall fit applied in the transition temperature region.

Since the vertical asymptotes are cut off by restricting the range for the tanh fit, approximate statistics.. c~_be Jierived in terms of temperature for specific energy values. A comparison of all three methods can then be performed to determine consistency and the most appropriate interval values.

For the upper shelf, the tanh fit gives an upper shelf level of (A+ B) which can be compared to the average value (mean value) for data points where the temperature is greater than or equal to (T0 + C). The statistics for the data in the upper shelf region can be calculated for both the mean value and for the level (A+ B). Consistency is expected except for spurious data or a defined upper shelf that does not match the majority of the upper shelf data.

4

The two most commonly used statistical bounds are the confidence and prediction intervals.

A confidence interval is a statistical interval about the mean regression equation at a

chosen probability level such that the regression falls within the bounds. A prediction interval is wider for the same statistical probability level and is a bound for predicting a future value of Y. _ The statistical probability levels of 68 % and 95 3 correspond closely to one and two sigma (estimated one and two standard deviation) levels and are commonly used. The confidence and prediction intervals are generally tighter near the model mean, and the intervals spread out in both directions away from the model mean. In some of the statistical calculations performed in the transition temperature region (T 0 + C), the intervals are artificially forced to spread away from the model mean even though more accurate statistical treatment may suggest constant values of the intervals; applying this approach is conservative moving away from the model mean. The student-t method is employed which takes into account the limitation of small sample sizes at appropriate statistical probability levels.

WELD WIRE HEAT W5214 UNIRRADIATED VESSEL AND THERMALLY-AGED STEAM GENERATORCVN DATAEVALUATION Weld wire heat W5214 exists in three pressurized water reactor (PWR) reactor pressure vessel surveillance programs: Indian Point Unit 2, Indian Point Unit 3, and H. B.

Robinson. All of these surveillance welds have had baseline Charpy data generated, and the energy results from these data are being analyzed and compared to the recent CVN results from the same weld wire heat in a* retired Palisades steam generator. This steam generator was in service for many years and may have experienced some aging at operating temperature.

All of the CVN data were analyzed using the tanh model for comparison.

The CVN values and the five curve fits are shown in Figures 3-7, and the tabulated CVN values are listed in Tables 1-4. The statistical evaluation details are shown in Appendix A for the overall fit, the transition temperature region, and the upper shelf. Tables

5 and 6 compare the statistical confidence intervals for 68 % and 95 % probability. These results are better shown graphically in Figures 8-13. For the 683 confidence intervals, the steam generator bounds fall outside the range of the surveillance weld bounds. At the 95 3 probability level, most of the ranges overlap except for some of the T50 results. The primary reason that the T30 bounds tend to overlap more is due to the flaring of the interval away from the model mean value. (T0

) which is very near T50

Therefore, the confidence interval results suggest that somewhere between a 683 and a 95% probability level, the steam generator CVN results are different from those for the surveillance welds (both individually and combined).

An alternative statistical view is to apply the student-t statistics to assess significance at the model mean values of T 0 and A using the regression tanh values and the associated standard deviations. Table 7 makes this comparison as well as a restatement of the 68%

confidence intervals for T30, T50, and (A+B). The last column defining statistical significance is the probability level for the student t value where the null hypothesis would 5

be violated indicating different values for the means between the steam generator material and" the surveillance welds. As suggested by the comparisons in Figures 8-13, the statistical level where the steam generator CVN results can be shown to be different from the surveillance weld results is clearly above the 68% level and on average near the 90% level for both transition temperature and energy.

In conclusion, at approximately a 90% probability level, the Palisades steam generator CVN data is different than any of the other CVN data from reactor pressure vessel surveillance programs for weld wire heat W5214.

6

Table 1: PALISADES STEAM GENERATOR DATA Temperature CVN Energy (F)

(ft-lbs)

-145 9.0

-80 20.7

-40 34.7

-40 20.3

-40 55.4 0

44.6 0

39.9 20 73.8 40 72.0 40 63.5 40 77.5 60 85.6 110 96.3 110 101.8 160 102.6 210 93.7

Table 2: INDIAN POINT UNIT 2 SURVEILLANCE DATA Temperature CVN Energy (F)

(ft-lbs)

-150 12.5

-150 10.5

-100 35.0

-100 9.0

-100 18.0

-80 13.0

-80 32.5

-80 26.0

-40 34.0

-40 35.5

-40 48.0 10 78.0 10 74.0 10 81.0 60 102.5 60 102.0 60 100.0 110 112.5 110 108.5 110 108.5 160 115.5 160 113.0 160 120.0 210 121.0 210 123.5 210 117.5

Table 3: INDIAN POINT UNIT 3 SURVEILLANCE DATA Temperature CVN Energy (F)

(ft-lbs)

-150 5.0

-150 2.0

-150 4.5

-100 29.0

-100 18.0

-100 25.5

-50 35.0

-50 33.0

-50 32.5

-35 78.0

-35 69.5

-35 54.5

-20 87.0

-20 82.0

-20 89.0 10 100.0 10 105.0 10 113.5 60 115.0 60 119.0 60 121.5 160 124.0 160 125.0 160 112.0

Table 4: H.B. ROBINSON SURVEILLANCE DATA Temperature CVN Energy (F)

(ft-lbs)

-150 19.0

-150 10.0

-150 30.0

-150 3.0

-150 34.5

-150 2.0

-100 38.0

-100 29.0

-100 25

-50 21.0

-50 54.5

-50 36.5 10 73.5 10 68.0 10 65.5 60 97.0 60 99.0 60 116.0 110 97.0 110 104.0 100 107.5 210 112.0 210 111.0 210 115.0

Table 5: Comparison ofW5214 Welds (68% Confidence Interval)

_ T30 Temperature Band Comparison (F)

DATA SET HIGH LOW MEAN Palisades Steam Generator

-36.9

-58.1

-47.5 Indian Point 2

-58.8

-74.4

-66.6 Indian Point 3

-60.7

-69.9

-65.3 H B Robinson

-99.7

-73.9

-86.8 Total Data*

-70.3

-85.7

-78.0 T50 Temperature Band Comparison (F)

DATA SET HIGH LOW MEAN Palisades Steam Generator 1.4 -13.2

-5.9 Indian Point 2

-23.9

-35.9

-29.9 Indian Point 3

-42.9

-49.5

-46.2 H B Robinson

-30.1

-48.3

-39.2 Total Data*

-38.9

-50.3

-44.6 Upper Shelf Energy Comparison (ft-lbs)

DATA SET HIGH LOW MEAN Palisades Steam Generator 108.5 99.5 104.0 Indian Point 2 122.5 117.5 120.0 Indian Point3 123.7 118.7 121.2 H B Robinson 123.0 111.8 117.4 Total Data*

118.4 114.6 116.5

Total Data Set is the combination of the Indian Point 2, Indian Point 3 and H B Robinson Data

Table 6: Comparison of W5214 Welds (95% Confidence Interval)

T30 Temperature Band Comparison (F)

DATA SET HIGH LOW MEAN Palisades Steam Generator

-25

-70

-47.5 Indian Point 2

-50.3 -82.9

-66.6 Indian Point 3

-ei5.5 -75.1

-65.3 H B Robinson

-114.3 -59.3

-86.8 Total Data*

-62.4 -93.6

-78.0 T50 Temperature Band Comparison (F)

DATA SET HIGH LOW MEAN Palisades Steam Generator 9.7 -21.5

-5.9 Indian Point 2

-17.4 -42.4

-29.9 Indian Point 3

-39.2 -53.2

-46.2 H B Robinson

-19.7 -58.7

-39.2 Total Data*

-33.2 -56.0

-44.6 Upper Shelf Energy Comparison (ft-lbs)

DATA SET HIGH LOW MEAN Palisades Steam Generator 116.0 92.0 104.0 Indian Point 2 125.5 114.5 120.0 Indian Point 3 127.0 115.4 121.2 H B Robinson 130.4 104.4 117.4 Total Data*

120.3 112.7 116.5

Total Data Set is the combination of the Indian Point 2, Indian Point 3 and H B Robinson Data

Table 7: Statistical Significance Comparison Confidence Intervals TANH Parameters Number of SIG vs. other data:

(68%)

(+/- Stmid. Dev.)

Data Statistical Significance T30 Tso A+B To A

Points Level Data Set (oF)

(of)

(ft-lb)

(oF)

(ft-lb) flr=n nuse tTo tA tuse SIG

-41.5

-5.9 104.0 0.0 53.l 11 4

+/- 10.6

+/- 7.3

+/-4.5

+/-23.l

+/-9.6 IP2

-66.6

-29.9 120.0

-12.3 61.1 15 9

82.7%

98.4%

100.0%

+/- 7.8

+/-6.0

+/-2.5

+/-21.3

+/-6.2 IP3

-65.3

-46.2 121.2

-36.6 61.7 12 6

100.0%

96.6%

100.0%

+/-4.6

+/-3.3

+/-2.5

+/- 10.1

+/-8.6 HBR

-86.8

-39.2 117.4

-18.8 59.8 11 6

90.4%

87.6%

99.6%

+/- 12.9

+/-9.1

+/-5.6

+/-27.2

+/-10.0 Combined

-78.0

-44.6 116.5

-30.9 59.4 36 27 99.5%

88.2%

100.0%

total

+/- 7.7

+/-5.1

+/- 1.9

+/-32.0

+/- 11.9 Compare SIG to IP2:

Compare SIG to HBR:

tTo = 1.40

=>

82.7%

tTo = 1.75

=>

90.4%

tA = 2.59

=>

98.4%

tA = 1.61

=>

87.6%

tuse = 8.41

=>

100.0%

tuse = 3.99

=>

99.6%

Compare SIG to IP3:

Compare SIG to Combined total:

lTo = 5.00

=>

100.0%

tTo = 2.97

=>

99.5%

tA = 2.27

=>

96.6%

tA = 1.59

=>

88.2%

tusE = 7.88

=>

100.0%

tuse = 10.15

=>

100.0%

w c.n 2

0 A

Q.

c.n w

a:

+B

-B

-C

+C To TEMPERATURE, T

(

T-To)

RESPONSE= A+ B Tanh C

Figure 1: Tanh CVN Curve

Temperature (°C)

-240

-129

-18 93 204 316 200~~~--~-.------..--~-..-----.-----.-~~-..-----.------.----.,271

0 150

£ e>

CD c CD

.c 100 0

0 c I >

>-e-m

.c.

50

(.)

Unirradiated --

Irradiated -

- 30_!!-lb -

- -lt---i-.I Lower shelf (brittle failure)

Upper shelf energy (USE)

(Ductile failure)

I I

I

/

/ ' t\\USE

/

50 ft-lb 203 136 68 Q L=====+/-:====::i=::+/-:=;:::j;::..=:~..+/-....::::___JL_ __ __!_ ____ J__ __ _J_ ____..l-__ _l o

-400

-200 0

200 400 600 Temperature (

0 f)

N93 0018 Figure 2: Typical Shift and Upper Shelf Energy Drop for Irradiation Ol Q) c Q)

.c u

0 c >

c.

ca

.c

(.)

Material: Linde 1092 SAW Heat No.: W5214 Upper Shelf Energy: 104.0 Lower Shelf Energy: 2.2 Fixed Temp. at 30 ft-lbs: -47.5 Temp. at 50 ft-lbs: -5.9 Tanh Curve Coefficients:

300 250 c

v N

B 200 n

e r

g 150 y

T L

B s 100 so 0

-300 A= 53.08 B = 50.88 c = 97.12 TO= 0.00 I*

1:.

~

c I

v(I

~!

I I

-200

-100 0

100 200 300 Temperature in Degrees P Figure 3: Palisades Steam Generator Data 400 500 600

Material: Linde 1092 SAW Heat No.: W5214 Upper Shelf Energy: 120.0

Lower Shelf Energy: 2.2 Fixed Temp. at 30 ft-lbs: -66.6 Temp. at 50 ft-lbs: -29.9 Tanh Curve Coefficients:

300 250 c v N

E 200 n

e r

g 150 y

F T

100 L

B s so 0

-300 A= 61.10 B = 58.90 c = 92.50 TO= -12.30 I I I

I l I I

I I

. Cl

.../ tr" t:I v

I J

1 c a

I I

-200

-100 0

100 200 300 Temperature in Degrees F Figure 4: Indian Point Unit 2 Surveillance Data 400 I

I I

I I I

I I

I 500 600

Material: Linde 1092 SAW Heat No.: W5214 Upper Shelf Energy: 121.2 Lower Shelf Energy: 2.2 Fixed Temp. at 30 ft-lbs: -65.3 Temp. at 50 ft-lbs: -46.2 Tanh Curve Coefficients:

300 250 c v N

E 200 n

e r

g 150 y

F T

100 L

B s so 0

-300 A= 61.70 B = 59.50 c = 48.30 TO= -36.60 l"I

~

0 I

_y I

I

-200

-100 0

100 200 300 Temperature in Degrees P Figure 5: Indian Point Unit 3 Surveillance Data 400 500 600

300 250 c v N

E 200 n

e r

g 150 y

F T

L B s 100 50 Material: Linde 1092 SAW Upper Shelf Energy: _ 117.4 Temp. at 30 ft-lbs: -86.8 Tanh Curve Coefficients:

A= 59.80 B = 57-.60 c/

8 10 0

-300

~-

c I

~ I I

I

-200

-100 0

Heat No.: W5214 Lower Shelf Energy: 2.2 Fixed Temp. at 50 ft-lbs: -39.2 C = 118.80 TO = -39.20

a.

~~

liil l;J I

iao 200 300 400 500 Temperature in Degrees F Figure 6: H. B. Robinson _Surveillance Data 600

c v N

Material: Linde 1092 SAW Heat No.: W5214 Upper Shelf Energy:.116.5 Lower Shelf Energy: 2.2 Fixed Temp. at 30 ft-lbs: -78.0 Temp. at 50 ft-lbs: -44.6 Tanh Curve Coefficients:

A= 59.36 B = 57.16 c = 82.87 TO= -30.94 250-f-'...,;_;_..;.;.:....~~;.;._~-+-.,..---',.....-;"'"+,...,..___,.;.;,...;.;.=.~...-;_,...:-_-+-.-.;.-~-+~-'----.:....-t--~~-I-;.;._~~

B 2.00~,...,.._..._,,~~"'-~+-~~-+...._.,..---'.;....;.;;.~.,..---'--'--+--'--~~~_:__--'-t--~~-1-~~-1 D

r 9 150-f-'.......,_....,...,..-""-i~---'-~+-~~"'+~--'-~~~"-'-"'+'----.;""--,.-""'+~--'---'-r'-~~-+-~-'----I y..

T 0---======---~~~~--~~--_..+;.........;...,.;;.+.....;, __ ~-----+------'

-300

-200

-100 0

100 200.

300 400 500 600 ir.. peratur* in Deqr*** P Figure 7: CQmbined Surveillance Weld Data

-~-

---~-----

-20

-30

-40

-50

-60

u. -e

I 1!

-70 G) a.

E G)

I-

-80

-90

-100

-110

-120

-47.5 +/- 10.6 Palisades Steam Generator T30 Temperature Band Comparison (68% Confidence Interval)

-66.6 +/- 7.8 Indian Point2

-65.3. +/- 4.6 Indian Point 3 Data Set

-86.8 +/- 12.9 HB Robinson

_7a n.,_ 7 7 Total Data*

Figure 8: T30 Temperature Band Comparison (68% Confidence Interval)

10 0

-10

-20

u. -

CD...

I -

-30 CIS...

CD Q.

E CD I-

-40

-50

-60

-70

-5.9 +/- 7.3 Palisades Steam Generator TSO Temperature Band Comparison (68% Confidence Interval)

-29.9 +/- 6.0 Indian Point 2

~

-46.2 +/- 3.3 Indian Point 3 Data Set

-39.2 +/- 9.1 HB Robinson

-44.6 +/- 5.7 Total Data*

Figure 9: TSO Temperature Band Comparison (68% Confidence Interval)

i

~ -

130 125 120 115 e> 110 G) c w

~

CJ 105

. 100 95 90 104 +/-4.5 Palisades Steam Generator Upper Shelf Energy Comparison (68% Confidence Interval) 120 +/-2.5 Indian Point2 121.2 +/- 2.5.

Indian Point 3 Data Set

~

117.4 +/- 5.6 HB Robinson 116.5 +/- 1.9 Total Data*

Figure 10: Upper Shelf Energy Comparison (68% Confidence Interval)

0

-20

-40

u. -

s !

-60 Cl)

Q.

E

~

-80

-100

-120

-47.5 +/- 22.5 Palisades Steam Generator T30 Temperature Band Comparison (95% Confidence Interval}

-66.6 +/.., 16.3 Indian Point2

-tib.3 +/- 9.8 Indian Point 3 Data Set

~

-86.8 +/- 27.5 HB Robinson

-78.0 +/- 15.6 Total Data*

Figure 11: T30 Temperature Band Comparison (95% Confidence Interval)

~

e

s -

t!

CD c.

E CD I-

-20

-5.9 +/- 15.6

-40 TSO Temperature Band Comparison (95°/o Confidence Interval)

-29.9 +/- 12.5

-44.6 +/- 11.4

-39.2 +/- 19.5

-80+---------..... ----------~*~--------~*----------..... --------.....

Palisades Steam Generator Indian Point 2 Indian Point 3 Data Set HB Robinson Total Data*

Figure 12: TSO Temperature Band Comparison (95% Confidence Interval)

140.0 130.0 120.0 In

5!

I = ->-e 110.0 Cl> c w

z >

0 100.0 90.0 80.0 104.0 +/- 12.0 Palisades Steam Generator Upper Shelf Energy Comparison (95% Confidence Interval) 120.0 +/- 5.5 121.2 +/- 5.8 116.5 +/- 3.8 Indian Point 2 Indian Point 3 Data Set 117.4 +/-13.0 HB Robinson Total Data*

Figure 13: Upper Shelf Energy Comparison (95% Confidence Interval)

APPENDIX A STATISTICAL EVALUATION DETAILS

Palisades Steam Generator CVN Evaluation (68% Statistical Intervals)

Summary: Complete data set, CVN vs. TANH A=

53.08 ft-lb C=

97.12 °F B =

50.88 ft-lb T0 =

0 °F*

T3o =

-47.5 °F Tso =

-5.9 °F T0 - C =

T0 + C =

Overall estimated standard deviation (se) for the tanh fit is +/-

Linear statistical fit, CVN = X, Temp = Y:

The estimated standard deviation (se) is +/-

Degrees of freedom are Statistical Interval = 68 %

Conf interval

-40.4 °F

+/- 10.3

-6.0 °F

+/- 7.1 Forced Linear fit, CVN = X, Temp = Y:

22.1 9

=>

OF

-97.12 °F 97.12 °F USE =

103.96 ft-lb 9.6 ft-lb t-factor = 1.05 Pred. interval

-40.4 °F

+/- 25.4

-6.0 °F

+/- 24.3 The estimated standard deviation (se) is +/-

Degrees of freedom are Statistical Interval = 68 %

21.4

°F Conf interval T3o:

-44.1 °F

+/- 9.8 Tso:

-5.9 °F

+/- 6.8 Forced Tanh fit, CVN = X, Temp = Y: **

The estimated standard deviation (se) is +/-

Degrees of freedom are Statistical Interval = 68 %

Conf interval T3o:

-47.5 °F

+/- 10.6 Tso:

-5.9 °F

+/- 7.3 Upper Shelf Energy, Temp = X, CVN = Y USE= A+ B:

The Se value is +/-

Degrees of freedom are Statistical Interval =

t-factor =

A+B USEbar 7.5 3

68%

1.19 ft-lb Conf interval 103. 96 ft-lb 98.6 ft-lb

+/-

4.5

+/-

2.6 A-1 10

= >

t-factor = 1.05 23.1 10

=>

op Pred. interval T3o:

-44.1 °F

+/- 24.5 Tso:

-5.9 °F

+/- 23.4 t-factor = 1.05 Pred. interval T3o:

-47.5 °F

+/- 26.4 Tso:

-5.9 °F

+/- 25.2 USE= USEbar The Se value is +/-

4.3 ft-lb Degrees of freedom are 3

Statistical Interval =

68 %

t-factor =

1.19 Pred. interval 103.96 ft-lb 98.6 ft-lb

+/-

10.0

+/-

5.7

Palisades Steam Generator CVN Evaluation (95 % Statistical Intervals)

Summary: Complete data set, CVN vs. TANH A=

53.08 ft-lb C=

97.12 °P B =

50.88 ft-lb T0 =

0 °P T3o =

-47.5 °F Tso =

-5.9 °P T0 -C =

T0 + C =

Overap. estimated standard deviation (se) for the tanh fit is+/-

Linear statistical fit, CVN = X, Temp = Y:

The estimated standard deviation (se) is +/-

Degrees of freedom are Statistical Interval = 95 %

Conf. interval T3o:

-40.4 °F

+/- 22.1 Ts0:

-6.0 °F

+/- 15.3 Forced Linear fit, CVN = X, Temp = Y:

The estimated standard deviation (Sc ) is +/-

Degrees of freedom are Statistical Interval = 95 %

Conf. interval

-44.1 °P

+/- 20.9

-5.9 °F

+/- 14.5 Forced Tanh fiJ, CVN = X, Temp = Y:

The estimated standard deviation (sc) is +/-

Degrees of freedom are Statistical Interval = 95 %

Conf. interval T30:

-47.5 °F

+/- 22.5 T50:

-5.9 °F

+/- 15.6 Upper SMl/ Energy, Temp = X, CVN = Y USE= A+ B:

The Se value is +/-

7.5 ft-lb Degrees of freedom are 3

Statistical Interval =

95 %

t-factor =

3.18 Conj. interval 22.1 9

=>

21.4 10

=>

23.1 10

=>

A+B USEbar.

103.96 ft-lb

+/-

12.0 98.6 ft-lb

+/-

6.8 A-2 op

-97.12 °P 97.12 °P 9.6 ft-lb USE =

103. 96 ft-lb t-factor = 2.26 op Pred. interval T3o:

-40.4 °F

+/- 54.7 Tso:

-6.0 °F

+/- 52.3 t-factor = 2.23 op Pred. interval T3o:

-44.1 °F

+/- 52.1 Tso:

-5.9 °P

+/- 49.9 t-factor = 2.23 Pred. interval T3o:

-47.5 °F

+/- 56.l Tso:

-S.9 °F

+/- 53.7 USE= USEbar The Sc value is +/-

4.3 ft-lb Degrees of freedom are 3

Statistical Interval =

95 %

t-factor = 3.18 Pred. interval 103.96 ft-lb 98.6 ft-lb

+/-

26.8

+/-

15;3

Indian Point Unit 2 Surveillance Weld CVN Evaluation (683 Statistical Intervals)

Summary: Complete data set, CVN vs. TANH A=

61.1 ft-lb C=

92.5 °F B =

58.9 ft-lb T0 =

-12.3 °F T

0 + C =

T3o =

-66.6 °F Tso =

-29.9 °F Overall estimated standard deviation (se) for the tanh fit is +/-

Linear statistical.fit, CVN-= X, Temp = Y:

The estimated standard deviation (se) is+/-

16.1

°F Degrees of freedom are 13

-104.8 °F 80.2 °F 6.2 ft-lb USE =

Statistical Interval =

68%

= >

t-factor = 1.03 Conf interval

-69.4 °F

+/-

5.2

-34.5 °F

+/-

4.3 Forced Linear fit, CVN = X, Temp = Y:

The estimated standard deviation (se) is +/-

Degrees of freedom are Statistical Interval =

68 %

Conf interval T3o:

-61.1 °F

+/- 6.3 Ts0:

-29. 7 °F

+/- 4.8 Forced Tanh fit, CVN = X, Temp = Y:

17.2

°F 14 Pred. interval

-69.4 °F

+/- 17.5

-34.5 °F

+/- 17.2

= >

t-factor = 1.03 Pred. interval TJo:

-61.1 °F

+/- 18.8 Tso:

-29.7 °F

+/- 18.4 The estimated standard deviation (se) is+/-

21.3

°F Degrees of freedom are 14 Statistical Interval =

68%

= >

t-factor = 1.03 Conf interval TJo:

-66.6 °F

+/- 7.8 Ts0:

-29.9 °F

+/- 6.0 Upper Shelf Energy, Temp = X, CVN = Y USE= A+ B:

Pred. interval T3o:

-66.6 °F

+/- 23.3 Ts0:

-29.9 °F

+/- 22.8.

USE= USEbar 120 ft-lb The Se value is +/-

Degrees of freedom are Statistical Interval =

t-factor =

7.2 8

68%

1.06 ft-lb The Se value is+/-

5.4 ft-lb Conf interval A + B 120 ft-lb

+/- 2.5 USEbar 115.6 ft-lb

+/- 1.9 A-3 120 115.6 Degrees of freedom are 8

Statistical Interval =

68 %

t-factor =

1.06 Pred. interval.

ft-lb

+/-

8.0 ft-lb

+/-

6.0

Indian Point Unit 2 Surveillance Weld CVN Evaluation (95 3 Statistical Intervals)

Summary: Complete data set, CVN vs. TANH A =

61.1 ft-lb C =

92.5 °P T0 - C =

-104.8 °P 80.2 °P USE=

120 ft-lb B =

58.9 ft-lb T0 =

-12.3 °P T0 + C =

T3o =

-66.6 °F Tso =

-29.9 °P Overall estimated standard deviation (Se) for the tanh fit is+/-

6.2 ft-lb Linear statistical fit, CVN = X, Temp = Y:

The estimated standard deviation (se) is +/-

Degrees of freedom are Statistical Interval = 95 %

Conf interval T3o:

-69.4 °P

+/-

10.9 Tso:

-34.5 °F

+/-

9.0 Forced Linear fit, CVN = X, Temp = Y:

The estimated standard deviation (Se ) is +/-

Degrees of freedom are Statistical Interval = 95 %

Conf interval

-61.1 "F

+/- 13.2

-29.7 °P

+/- 10.1 Forced Tanh fit, CVN = X, Temp = Y:

The estimated standard deviation (se) is +/-

Degrees of freedom are Statistical Interval =

95 %

Conf interval T30:

-66.6 "F

+/- 16.3 Tso:

-29.9 "F

+/- 12.5 Upper Shelf Energy, Temp = X, CVN = Y USE= A+ B:

The Se value is +/-

Degrees of freedom are Statistical Interval =

t-factor =

7.2 8

95%

2.31 ft-lb Conf. interval A + B 120 ft-lb

+/- 5.5 USEbar 115.6 ft-lb

+/- 4.1 16.1

°F 13

= >

t-factor = 2.16 17.2

°P 14 Pred. interval T3o:

-69.4 °P

+/- 36.5 Tso:

-34.5 °F

+/- 36.0

= >

t-factor = 2.14 Pred. interval T3o:

-61.1 °P

+/- 39.2 Ts0:

-29.7 "F

+/- 38.2 21.3

°F 14

= >

t-factor = 2.14 A-4 Pred. interval T30:

-66.6 "F

+/- 48.5 Tso:

-29.9 °F

+/- 47.3 USE= USEbar The Se value is+/- 5.4

ft-lb Degrees of freedom are 8

Statistical Interval = 95 %

t-factor = 2.31 Pred. interval 120 ft-lb

+/- 17.4 115.6 ft-lb

+/- 13.1

e I

Indian Point Unit 3 Surveillance Weld CVN Evaluation (683 Statistical Intervals)

Summary: Complete data set, CVN vs. TANH A=

61.7 ft-lb C=

48.3 °F B =

59.5 ft-lb T0 =

-36.6 °F T3o =

-65.3 °F Tso =

-46.2 °F Overall estimated standard deviation (se) for the tanh fit is+/-

Linear statistical fit, CVN = X, Temp = Y:

The estimated standard deviation (s0 ) is +/-

Degrees of freedom are Statistical Interval = 68 %

Conf interval

-56.5 °F

+/- 4.9

-41.4 op

+/- 3.4 Forced Linear fit, CVN = X, Temp = Y:

The estimated standard deviation (s0 ) is +/-

Degrees of freedom are Statistical Interval = 68 %

Conf interval

-62.3 °F

+/- 4.2

-46.1 °P

+/- 3.0 Forced Tanh fit, CVN = X, Temp = Y:

The estimated standard deviation (s0 ) is +/-

Degrees of freedom are Statistical Interval = 68 %

Conf interval T30:

-65.3 °F

+/- 4.6 Tso:

-46.2 °F

+/- 3.3 Upper Shelf Energy, Temp = X, CVN = Y USE= A+ B:

The s0 value is +/-

5.5 ft-lb Degrees of freedom are 5

Statistical Interval =

68%

t-factor =

1.10 Conf interval A+B 121.2 ft-lb

+/-

USEbar 119.4 ft-lb

+/-

2.5 2.3 A-5 8.7 10

=>

9.2 11

=>

10.1 11

=>

-84.9 °F 11.7 °F USE =

121.2 ft-lb OF OF 8.6 ft-lb t-factor = 1.05 Pred. interval T30:

-56.5 °F

+/- 10.3 Tso:

-41.4 °P

+/- 9.7 t-factor = 1.04 Pred. interval T30:

-62.3 °F

+/- 10.4 Tso:

-46.1 °P

+/- 10.0 OF t-factor = 1.04 Pred. interval T3o:

-65.3 °F

+/- 11.5 Tso:

-46.2 °P

+/- 11.0 USE= USEbar The s0 value is +/-

5.1 Degrees of freedom are 5

Statistical Interval =

68%

t-factor =

1.10 Pred. interval 121.2 ft-lb

+/-

6.5 119.4 ft-lb

+/-

6.1 ft-lb

Indian Point Unit 3 Surveillance Weld CVN Evaluation (95 % Statistical Intervals)

Summary: Complete data set, CVN vs. TANH A=

61. 7 ft-lb C=

48.3 °F B =

59.5 ft-lb T0 =

-36.6 °F T30 =

-65.3 °F Tso =

-46.2 °F T0 - C =

T0 + C =

Overall estimated standard deviation (sc) for the tanh fit is+/-

Linear statistical fit, CVN ::= X, Temp = Y:

The estimated standard deviation (sc) is +/-

Degrees of freedom are Statistical Interval =

95 %

Conj. interval.

T3o:

-56.5 °F

+/- 10.4 Ts0:

-41.4 °F

+/- 7.3 Forced Linear fit, CVN = X, Temp = Y:

The estimated standard deviation (sc) is +/-

Degrees of freedom are Statistical Interval =

95 %

Conf interval T3o:

-62.3 °F

+/- 8.9 Tso:

-46.1 °F

+/- 6.3 Forced Tanh fit, CVN = X, Temp = Y:

The estimated standard deviation (sc) is +/-

Degrees of freedom are Statistical Interval = 95 %

Conj. interval

-65.3 °F

+/- 9.8

-46.2 °F

+/- 7.0 Upper Shelf Energy, Temp = X, CVN = Y USE= A+ B:

The Sc value is +/-

Degrees of freedom are Statistical Interval =

t-factor =

5.5 ft-lb 5

95%

2.57 Conj. interval A+B USEbar 121.2 119.4 ft-lb

+/-

ft-lb

+/-

5.8 5.4 8.7 10

=>

9.2 11

=>

10.1 11

=>

A-6

-84.9 °F 11.7 °F USE = 121.2 ft-lb OF

°F 8.6 ft-lb t-factor = 2.23 Pred. interval T3o:

-56.5 °F

+/- 22.0 Tso:

-41.4 °F

+/- 20.7 t-factor = 2.20 Pred. interval T3o:

-62.3 °F

+/- 22.1 Tso:

-46.1 °F

+/- 21.1

°F t-factor = 2.20 Pred. interval

- T3o:

-65.3 °F

+/- 24.3 Tso:

-46.2 °F

+/- 23.3 USE= USEbar The Sc value is +/-

5.1 Degrees of freedom are 5

Statistical Interval =

95%

t-factor = 2.57 Pred. interval 121.2 ft-lb

+/-

15.2 119.4 ft-lb

+/-

14.2 ft-lb

H. B. Robinson Surveillance Weld CVN Evaluation (683 Statistical Intervals)

Summary: Complete data set, CVN vs. TANH A=

59.8 ft-lb C = 118.8

°P

-137.6 "F 100 °P

USE =

117.4 ft-lb B =

57.6 ft-lb T0 = -18.8

°P T0 + C =

T3o =

-86.8 "F Tso = -39.2

°P Overall estimated standard deviation (s.) for the tanh fit is +/-

Linear statistical.fit, CVN = X, Temp = Y:

The estimated standard deviation (s.) is+/-

Degrees of freedom are Statistical Interval =

68 %

Conf interval T3o:

-78.3 °P

+/- 10.5 Ts0 :

-37.8 "F

+/- 7.8 Forced Unear fit, CVN = X, Temp = Y:

10.0 ft-lb 24.1

°P 9

= >

t-factor = 1.05 Pred. interval T3o:. -78.3 "F +/- 27.4 Ts0:

-37.8 "F +/-

26.5 The estimated standard deviation (s.) is+/-

22.9

°P Degrees of freedom are Statistical Interval =

68 %

Conf interval T3o:

-80.3 "F

+/-

10.9 Tso:

-39.0 °P

+/- 7.7 10

=>

t-factor = 1.05 Pred. interval T3o:

-80.3 "F +/-

26.3

- Tso:

-39.0 "F +/-

25.l Forced Tanh fit, CVN = X, Temp = Y:

(Note that this data set was evaluated by eliminating one data point near the upper shelf)

The estimated standard deviation (s0 ) is +/-

Degrees of freedom are Statistical Interval =

68 %

Conf interval T3o:

-86.8 "F

+/-

12.9 Tso:

-39.2 "F

+/- 9.1 Upper Shelf Energy, Temp = X, CVN = Y USE= A+ B:

The s. value is +/-

Degrees of freedom are Statistical Interval =

t-factor =

12.4 5

68%

1.10 ft-lb Conf interval A+B USEbar 117.4 ft-lb

+/-

5.6 107.8 ft-lb

+/-

2.9 A-7 27.2 "F

10

= >

t-factor = 1.05 Pred. interval T3o:

-86.8 "F +/-

31.2 Tso:

-39.2 °P * +/-

29.9 USE= USEbar The s0 value is +/-

6.5 Degrees of freedom are 5

Statistical Interval =

68%

t-factor =

1.10 Pred. interval 117.4 ft-lb

+/-

14.8 107.8 ft-lb

+/-

7.7 ft-lb

H.B. Robinson Surveillance Weld CVN Evaluation (95% Statistical Intervals)

Summary: Complete data set, CVN vs. TANH A=

B=

59.8 ft-lb 57.6 ft-lb C = 118.8

°P T0 -C =

T0 + C =

-137.6 °P 100 °F USE=

117.4 ft-lb T0 = -18.8

°F T3o =

-86.8 °P Tso = -39.2

°F Overall estimated standard deviation (s.) for the tanh fit is+/-

10.0 ft-lb Linear st.Jtistical fit, CVN = X, Temp = Y:

The estimated standard deviation (se) is +/-

24.1

°F Degrees of freedom are 9

Statistical Interval =

95%

= >

t-factor = 2.26 Conf. interval T3o:

-78.3 °F

+/- 22.7 Ts0:

-37.8 °F

+/-

16.7 Forced Linear fit, CVN = X, Temp = Y:

The estimated standard deviation (se) is+/-

22.9

°f Degrees of freedom are 10 Pred. interval T3o:

-78.3 °P

+/-

59.0 Tso:

.-37.8 °P +/-

57.0 Statistical Interval = 95 %

= >

t-factor = 2.23 Conf. interval T3o:

-80.3 °P

+/- 23.2 Ts0:

-39.0 °F

+/-

16.4 Forced Tanh fit, CVN = X, Temp = Y:

The estimated standard deviation (Se ) is +/-

Degrees of freedom are Statistical Interval =

95 %

Conf. interval T30:

-86.8 °F

+/- 27.5 Tso:

-39.2 °F

+/-

19.5 Upper Shelf Energy, Temp = X, CVN = Y USE= A+ B:

The Se value is +/-

Degrees of freedom are Statistical Interval =

t-factor =

12.4 5

95%

2.57 ft-lb Conj. interval Pred. interval T3o:

-80.3 °P +/-

56.0 Tso:

-39.0 °F +/-

53.5 (Note that this data set was evaluated by eliminating one data point near the upper shelf) 27.2

°P 10

= >

t-factor = 2.23 Pred. interval T3o:

-86.8 °F +/-

66.5 Tso:

-39.2 °P +/-

63.6

USE = USEbar The Se value is +/-

6.5 Degrees of freedom are 5

Statistical Interval =

95%

t-factor =

2.57 Pred. interval A+B USEbar 117.4 ft-lb

+/-

13.0 117.4 ft-lb

+/-

34.4 107.8 ft-lb

+/-

6.8 107.8 ft-lb

+/-

18.0 A-8 ft-lb

Combined Surveillance Weld CVN Evaluation (68% Statistical Intervals)

Summary: Complete data set, CVN vs. TANH A =

59.36 ft-lb C =

82.87 °P T0 - C =

-113.81 °F 51.93 °F USE =

116.52 ft-lb B =

57.16 ft-lb T0 =

-30.94 °P T0 + C =

T30 =

-78.0 °F Tso =

-44.6 °F Overall estimated standard deviation (se) for the tanh fit is+/-

linear statistical fit, CVN = X, Temp = Y:

The estimated standard deviation (se) is +/-

Degrees of freedom are Statistical Interval =

68 %

Conf interval T30:

-71.8 °F

+/- 4.6 Ts0:

-47.1 °F

+/- 3.7 Forced Linear fit, CVN = X, Temp = Y:

11. 9 ft-lb 22.0

°F 34

= >

t-factor = 1.01 Pred. interval T3o:

-71.8 °F +/- 22.7 Tso:

-47.1 °F +/-

22.5 The estimated standard deviation (se) is +/-

22. 7

°F Degrees of freedom are 35 Statistical Interval =

68%

= >

t-factor = 1.01 Conf interval T30:

-73.5 °F

+/- 5.5 Ts0:

-44.5 °F

+/- 4.0 Forced Tanh fit, CVN = X, Temp = Y.*

The estimated standard deviation (se) is+/-

Degrees of freedom are Statistical Interval =

68 %

Conf interval T3o:

-78.0 °F

+/- 7.7 T50:

-44.6 °F

+/- 5.7 Upper Shelf Energy, Temp = X, CVN = Y USE= A+ B:

The Se value is.+/-

Degrees of freedom are Statistical Interval =

t-factor =

A+B USEbar 9.7 26 68%

1.01 ft-lb Conf interval 116.52 ft-lb

+/-

111.8 ft-lb

+/-

1.9 1.7 A-9 32.0

°P 35 Pred. interval T30:

-73.5 °F +/- 23.6 Tso:

-44.5 °F +/- 23.3

= >

t-factor = 1.01 Pred. interval T30:

-78.0 °F +/-

33.2 Tso:

-44.6 °F

+/-

32. 7 USE = USEi,ar The Se value is +/-

8.5 Degrees of freedom are 26 Statistical Interval =

68%

t-factor =

1.01 Pred. interval 116.52 ft-lb

+/-

10.0 111.8 ft-lb

+/-

8.8 ft-lb

Combined Surveillance Weld CVN Evaluation (953 Statistical Intervals)

Summary: Complete data set, CVN vs. TANH A =

59.36 ft-lb c =

82.87 °F T0 - C =

-113.81 °P 51.93 °F USE =

116.52 ft-lb B =

57.16 ft-lb T0 =

-30.94 °F T0 + C =

T3o =

-78.0 °F Tso =

-44.6 °F Overall estimated standard deviation (se) for the tanh fit is+/-

11.9 ft-lb Linear statistical fit, CVN = X, Temp = Y:

22.0

°P 34 The estimated standard deviation (sc) is +/-

D~grees of freedom are Statistical Interval =

95 %

= >

t-factor = 2.03 Conf interval

-71.8 °F

+/- 9.3

-47.1 °F

+/- 7.5 Forced Linear fit, CVN = X, Temp = Y:

The estimated standard deviation (sc) is+/-

22.7

°F Degrees of freedom are 35 Pred. interval

-71.8 °P +/-

45.7

-47.1 °F +/-

45.3 Statistical Interval =

95 %

= >

t-factor = 2.03 Conf interval T3o:

-73.5 °F

+/-

11.1 Tso:

-44.5 °F

+/- 8.1 Forced Tanh fit, CVN = X, Temp = Y:

Pred. interval T3o:

-73.5 °F +/- 47.5

_ Tso:

-44.5 °F +/-

46.9 The estimated standard deviation (sc) is +/-

32.0

°F Degrees of freedom are 35 Statistical Interval =

95%

= >

t-factor = 2.03 Conf interval Pred. interval T3o:

-78.0 °F

+/-

15.6 T3o:

-78.0 °F +/- 66. 7 Tso:

-44.6 °F

+/- 11.4 Tso:

-44.6 °P +/-

65.9 Upper Sh*lf Energy, Temp = X, CVN = Y USE= A+ B:

USE= USEbar The Sc va!ue is +/-

9.7 ft-lb The Sc value is +/-

8.5 Degrees of freedom are 26 Degrees of freedom are 26 Statistical Interval =

953 Statistical Interval =

95%

t-factor =

2.06 t-factor =

2.06 Conf interval Pred. interval A+B 116.52 ft-lb

+/-

3.8 116.52 ft-lb

+/-

20.4 USEbar 111.8 ft-lb

+/-

3.4 111.8 ft-lb

+/--

17.7 A-10 ft-lb

ATTACHMENT NO. 4 Consumers Power Company Palisades Plant Docket 50-255 RESPONSE TO NRC NOVEMBER 30,1994 REQUEST FOR ADDITIONAL INFORMATION REVIS ION 1 10CFRS0.61 SCREENING CRITERION ITEM NO. 4 There are np changes from Revision 0.

15 Tables 4 Figures

TABLE 4-l

!ABLE 3.

CHAR.PY V-NO'l'CH Il-1PACT RESU1.':S :"OR BASE ME:AL PLATE NO. 03803-t, LJNGiruD~AL OR!.::N!A:"ICN

!mp ac c:

Lac:eral Specimen Temperac:ure,

Energy, Expansion, No.

or fc:-lb mils l4E

-150 2.0 2.0 147

-100 3.0 4.5 145

-33 lO.O 12.0 l4D

-15 15.5 19.0 l4C

+5 34.0 33.5 143

+21 49.0 45.0 171

+49 77.5 63.0 172

+49 67.0 54.5 173

+49 90.0 67.0 146

+SO 69.0 56.0 141

+72 94.0 75.0 14A

+llO 129.5 88.0 142

+150 135.5

93. 5 14B

+225 162.5 85.5 144

+294 143.0 94.0 l4J

+360 178.0 78.0 Fracc:ure Appearance, Percent Shear 0

0 l

5 10 15 25 20 25

25.

so 80 100 100 100 100

r.::...nLC: 4-2

!ABLE 4.

CHAR~Y V-NO'l'CH !}!PACT RESUL!S FOR BASE ~E'!...1.L PU!!

NO. D3 803-1, ntANSVERS E OR!EN!A TION Imp ac: c Laceral F rac :ure Specimen Temperacure,

Energy, Expansion, Appea:-ance, No.

'"F fc-lb mils Percenc Shear 23P

-150 2.0 2.5 0

21E

-100 4.0 4.0 o

2lB

-33 ll.O 13.s 2

23M

-15 12.0 16.0 5

23L

+5 41.5 38.5 10 217

+21 2 7.o 29.0 15 2lD

+SO 46.0 44.0 20 215

+72 60.0 53.5 30 23T

+90 68.5 58.0 50 23J

+110 94.0 75.0 so*

216

+150 114.0 79.0 100 23K

+22.5 107.o 79.0 100 2U

+295 92.0 75.5 100 252

+296 102.0 81.5 100 23U

+360 93.o 78.0 100 9

t:h..JL!.: 4-3 TABLE S.

CHAR.PY V-NO'I'Ca D1PAC! RESUL:'S FOR :.IE:LD ME'!AI.

Impacr:

Lateral Ft:"acr:ure Spee imen Temperat11re,

Energy, Expansion, Appearance, No.

ft-lb mils Percent Shear 36?

-170 4.0 s.o 0

36J

-150 7.0 7.0 0

36P

-135 14.5 14.5 2

367

-100 a.s ll.O 1

36M

-100 3 l.O 28.0 5

36L

-85 3 s.o 33.5 10 36!

-75 47.5 41.0 15 360

-so 41.0 39.0 20 365

-33 56.0 S2.0 30:

36C

-s 87.0 75.0 60 363

+20 86.0 77.o 80 366

+SO 92.0 79.0 80 361

+72 96.0 as.a 90 36A

+llO 117.s 94.0 100 362

+150 112.0 88.5 100 36B

+225 127.5 92.0 100 364

+296 lll.O 87.0 100 35K

+360 120.5 91.5 100

T.. -\\..U.L...i::.:.-4 TABLE 6.

CHAR.PY V-NO!CH D!PACT RESU!.!S FOR CZ.AZ !-!.ET.AL Impa.c: t Laceral Frac:~:-e Spec:imen Temperature, EnerSY.

Expa.nsia:i,

.Appearanc.e, No.

OF.

ft-tb t:'\\ilS Percent, Shear 47Y

-170 s.o 4.0 0

471

-150 s.o 3.0 0

43A

-145 6.0 s.o 0

475

-137 6.0 3.5 2

474

-135

13. fJ 10.0 l

473

-120 15.0 ll.O 5

476

-109 20.0 ts.a 5

477

-101 25.0 18.5 10 467

-100 64.0 43.0 15 4lA

-75 13.o l3.5 5

465

-34 76.s 56.0 40 463

+20 77.0 45.S so 466

+SO 94.0

?l.O 85 461

+72 112.0 76.5 80 46A

+llO 90.0 74.0 100 462

+lSl 114.0 81.0 100 46C

+225 120.0 86.0 100 464

+296 138.s 87.0 100 472

+360 llS'.O 75.0 100

Sample No.

22M 22L 22J 22E 21L 228 22C 21J 2lK 220 22!<

21M CAPSULE T-330, THERMAL CAPSULE CHARPY V-NOTCH IMPACT DATA FOR THE PALISADES INTERMEDIATE SHELL PLATE D-3803-1 (TRANSVERSE ORIENTATION)

Temperature Impact Energy Lateral Expansion (oF)

(ft-lb)

(mils)

-75 5

6.5

-25 13 18 25 28 20 50 47 42.5 60 48 47.5 77 79 58 100 71 60 150 82 64.5 200 112 78 250 92 74 300 117 80 400 110 78 Shear

(%)

5 10 26

. 47 45 50 56 78

o 180 100

~00

CAPSULE T-330, THERMAL CAPSULE CHARPY V-NOTCH IMPACT DATA FOR THE PALISADES INTERMEDIATE SHELL PLATE D-3803-1 (LOHGlTUOINAL ORIENTAtION)

Sample Temperature Impact Energy Lateral Expansion No.

(oF}

(ft-lb)

(mils}

13M

-so 7

9 13P 0

13 13.S 13C 25 39 32.S 13B 35 so 47.2 13E so 65 53 13J 77 112 74.S 131<

lSO 131 9l.S 13Y 2QO 156 87.0 130 300 158

77. s l3L 350 158 85.S UT 400 215 67.S TSpecimen :3U ~as improperly centered on anvil.

3C929: lb-091384 Shear

(%)

2 14 20 27 40 56 83 lQO

oo

~00

oo

Sample No.

33M 33K 343 341 33L 33P 342 33Y 344 33T 33J 33U L\\rlLE <;.- 7 CAPSULE T-330, THERMAL CAPSULE CHARPY V-NOTCH IMPACT DATA FOR THE PALISADES PRESSURE VESSEL WELD METAL T~rature Iq>act Energy Lateral Expansion (oF)

(ft-lb)

(mi ls)

-100 12 17

- 75 45 39

- 60 22 26

- so 31 32

- so

.23 26

- 25 32

. 28. 5 0

82 65.5 25 93 75.5 77 79 88.S 150 120 94.5 300 122 74.5 350 155 79 3CS23:lb*C91384 Shear

(%)

18 30 29 37 42 40 60 84 94

.JQ

oo

Sample No.

430 420 42E 440 43E 41E 46E 44E 460 45~

410 450 CAPSULE T-330, THERMAL CAPSULE CHARPY V-NOTCH IMPACT OATA FOR THE PALISADES PRESSURE VESSEL WELD HEAT-AFFECTED ZONE METAL Temperature Impact Energy Lateral Expansion (oF)

(ft-lb)

(mi ls)

-75 45 39

-25 27 27.5

-10 43

41. 5 o

55 47.5 25 52 47 40 88 57 so 130 84 60 115 81 77 70 55 1,50 125

90.5 225 110 67 300 121 77 8C929:::-091984 Shear

(%-)

3 14 34 44 43 62 88 34 85

"II'\\

..J\\J

80 100

LO C)

'° N

Ol u

0

'°

~

'° CXl

~

s.., **

llumbar 22H 22L 2U 221 21L 221 22C 2 IJ 211 220 221 21H Teet T**P

( *>

-n

-n 2S so 60 11 100 ISO 200 no lOO 400 Clal"pJ

'fAllLt: 4-9 CAPSU1£ T-330. Jtl[llMAL CAPSULE INSIHUM£Hl£0 CllAHPY IMPACT IESI RESULIS FOR PAL I SADES IHURNEOIATE SUELL PLAIE 0-3003-1 (IRAHSVERSE OllUNIATIO.)

lloraallaed lne.-11**

a.un lla*l*um r.-op lleH Tt..

llad*um

..,...,. Ip/A Load to ltald Lo.cl (ft *~*> :-----

(ft-l~*/l*A2)

(Up*)

(ulec)

(Upe) s.o 40 11 21 2.60 n.o 10'1 JO 14

].}()

o l.SS 21.0 22S 119 81 1.10 IS 1.n 41.0 lJI 191 110 2.H 160 l.9S 48.0

)IJ 2S4 111 1.95 IS l.9S 19.0 616

)OJ

)29

2.n 10 4.00 JI.o U2 262 109 2.60

o l.IS 12.0

'60 191 461 2.JO 10 1.60 IU.O tOJ 2S8 644 2.60 IS 1.n

2.0 141 226 SIS 2.n 50 l.SO 111.0

42 294 641 2.10 so

].'S'S 110.0 116 249

'11 2.10 H

l.U 1

TIM to r.-*clure Aneet Yield rlo11

....a....

Load Load fill"e**

Su****

(ulec)

(Up*)

(li.lpe)

(.... 1)

IS 2.60 an J.SS

.2S I08 111 no J.n

.JO I02 111 uo 1.n a.n 114 60S

].90 I.SS 98 an Jl'j J.IS 1.n 94 1 ll 6SS

].60 I.ts 16 IOI 500

).00 2.so 89 I04 6SS 16 IOS 610 14 9S 11'1 69 91 1J t4

u OU 89 SOI H

01 UL

'IOI

\\8 UI

\\01 OL 0 I O{"l Sit (6

ot* 1 u*c Sit

\\II l6 o**

u*c Ott Oii

\\i

\\l"l u*c Olt 66 OL"

\\O"t Ht

\\01 tOI u*

01 *c Sll 01*

u*c

\\I (1*~)

(1*~)

<.. n>

<*dn)

(391")

- - l1S

- - .119 P901 p*oi mn*PWM

.. o..

Pt*ll,......, *Jn1:>*J*

01.. 11 o~*'

Ot 01*z ttt1 Ht IU1 0*~1t n*t St 01*z HE uu 0*1s1

\\\\"t 001 ot*z lH OH UZ1 O"IS1 u*t

°'

n*z cu nc tHI O"HI o**c Ot n*z UL UC

\\~01 O" ICI Ol"t 01 Ol"l lni\\

OU ZOI o*zn oo*t o*

o**z iOE tll tn o*n Ot"C 01 H"l ltl n1 tot O"O\\

\\O"t

\\I oo*c IOZ ti(

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Ol"(

o*

\\I "t It

~01 o*u n*t lt tl t\\

o*t c.. n>

(......,

I' (3-Sft).

cz.*11.W.1-11> -----

c*~*,,,

.,.... 111 P901 pt*U 01 P901 mn*PWM

.. 11 do.1*....,.... HH'I:)

- 1l.1.u1, **,,......

(J<<JllYINJlllO 1YNIOflll!Jflll) 1-£00£-0 llYld llJHS llYIOJtQIJJNI SJOVSI lVd HOJ SJ lOSJll lSU lJVdtU AdHV111 OJlNJtlUllSNI

]lOSdYJ lVIQl]IU

on: -J JlOSdVJ 01 _., :*rrnv.1.

'd.Jeq:)

oot OU 00(

OOl 0\\1 LL OS u u 0

OS-u) 1**1 IU

,(1 au All **

fll Ill Ill

>Cl

Cl MCI J~

tdns m

N 0 rn

(Jj C>

<D N

lJ]

u -

0

<D

())

~

s-,**

llH 111l 10 141

))L llP 142 l11 lU lJT 1lJ llU Teet T-p

( r)

-100

-n

-60

-so

-H 0

n 11 no 100 no ChHPJ

'fABl.~ 4-ll CAPSULE I -330. 1 llERMAL CAPSULE INS1RUN£Nl£0 CllARPY IMPACT TEST RESULTS FOR PALISADES WELD METAL 11o.... 1taed Ener1l**

a....,, 11a.a...

Prop 11e14 Tl..

llaal*ua la/A Ip/A Lo**

to llel*

Lo..

(ft l~a) -----

(ft-l~e/ta*J)

(U,.)

(ulec)

(kip*)

u.o tJ 61 2t J.H an J.H o.o JH 211 144 1.U to

4. lS n.o 111 n*

11 1.1, 95 1.H ll.O HO 116 14 J.H H

1.H 21.0 ll!i 104 H

1.n to

).JO u.o JSI Ill 11 J.H H

1.H 12.0 HO HO 111 1.10 to 4.10 tl.O J4t 214 414 2.H H

1.to Jt.O

'16 l)S 101 2.10 H

).10 120.0 100 2.so n

l.65 122.0 tl2 211 2.20 n

1.40 us.o U41 110 2.ao 65

).JO Tt.. to fracrure Arre et Yield Flow 11aa1-Load Loe4 Str***

Str***

(ulec)

(Ii.Ip*)

(Upa)

(hi)

(hi) 200 1.10

.10 121 ll4 500 4.0S

IS llO 121 10 l.IS

.o 110 4H l.n

.so 101 210

).SS

.,,s IOI an 40 l.10

.n lOS 116 610

).0.

I.IS 102 nt 1.40 2.2 91 I U IH 2.n 2.2 90 101 110 ll 102 110 11 tl JH JO to

LO 0

tD N

CD rr 0

'°

'° Ol

~

s-p**

llhmMr UD UD 421 440 411 411 461 441 4'D UI 41D UD Te*t T**P

( *>

-n

-10 0

u 40 so

'° 11 ISO JH 100

<llerpr lnerar

'l'AliLE 4-12 CAPSULE T-330, THEllNAL CAPSULE INSTllUMENIEO CHARPY IMPACT TEST RESULTS FOR PALISADES WELD HEAT AFFECTED ZlltE METAL llor.all*ed !ner1l**

O*r*r........

Pl"op 11eld Tt..

tleal*Ull Ip/A Loa*

to 11a1*

Load (It l~a) ----- (ft-lllta/l**J)

(kl pa)

(ulec)

(kl pa) 11.0 111 114 21 l.SS H

4.0S 11.0 HJ 114 44 1.40 IOS 4.0S u.o 14' UJ IU 1.14 to 4.U

. ss.o 441 IH 264 l.SO IOS 4.U sz.o 41t 211 201 1.20 "to 1.to 11.0 JOI 14J 162 1.U to 4.10 uo.o IOU 126 121 1.10 ts 4.10 au.o tJ6 212

H 1.IS 100 4.00 JO.O SH 2ot U4 1.0S H

4.00 an.o IOOJ

)I)

'91 2.10 H

).JS 110.0 116 24' 640 2.4' H

1.10 Ul.O JU

.. 2 2.25 H

).,,

Tl.. to rraclul"* An**t lleld flo11 Load Load Stl"e**

s,.....

(ulec)

(Up*)

(lklpe)

(hi)

(hi) 2n 4.0S 111 IH 410 4.0S

.u 112 IU sos 4.U 1.n 110 124 41S

4. IS

.n 116 121

~

1.10 a.u

106 Ill 110 1.n 1.n IOS 124 JSO

Z. IS 1.40 101 119 "s

Z.10 1.60 101 Ill us 1.H 2.u lOl 111 JJO 92 108 610 10 101 120 14

Weld Palisades surveillance weld Palisades HAZ weld I

Best Estimate TABLE 4-13 CHEMISTRY FOR WELDS FABRICATED WITH RACO 3 WELD WIRE HEAT NUMBER 3277 WITH Ni200 NICKEL ADDITION Copper (%)

Nickel (%)

Phosphorus (%)

Content Mean Content Mean Content Mean 0.26 0.25 0.63 1.36 0.011 0.014 0.22 1.27 o.011 0.25 1.60 0.013 0.30 1.38 0.014 0.239 1.617 0.016 0.231 1.502 0.017 0.. 233 1.494 0.017 0.25 0.25 0.43 1.09 0.011 0.013 0.20 1.28 0.012 0.26 1.19 0.015 0.25 0.95 0.014 0.26

1. 25 0.013 0.27 0.98 0.014 0.26

1. 27 0.014 0.23 1.09 0.012 0.27 0.90 0.014 0.23 1.18 0.012 0.22 1.28 0.012 0.22 1.27 0.012 0.28 1.02 0.014 0.22 1.10 0.012 0.27 1.22 0.015 0.28 0.94 0.015 0.27 1.18 0.015 0.23 0.89 0.012 0.27 0.92 0.014 0.26 1.15

0. 011 0.21 1.29 0.013 0.22

1. 31 0.012 0.27 1.02 0.014 0.23 1.12 0.012 I

I 0.25 I I

1.22 I I

0.014 I

TABLE 4-14 PALISADES REACTOR VESSEL SURVEILLANCE PLATE CHEMISTRY Material Copper (%)

Nickel (%)

Phosphorus (%)

D-3803-1 0.22 0.49 0.010 0.25 0.48 0.013 0.24 0.53 0.011 0.24 0.53 0.005 0.215 0.52 0.004 0.215 0.523

<0.013 0.215 0.496

<0.013 0.495

<0.013 Best Estimate 0.23 0.51

<0.010

Cycle 1

2 2

2 3

4 5

6 7

8 9

10 11 Steam Generator and PCS Data-Cycles 1 thru 11 TABLE 4-15 Typical Typical Typical Typical Dates Hours Critical Power SG Pressure SG Temp T-inlet 12/30/71-12i20t75 16,087 70 670 498 523 05i18176-04; 18177 7,722 100 615 489 522 04/ 19/77-11, 06177 4,351 100 660 497 529 11/07177-01/06/78 1.508 100 690 502

. 535 04i22/7 8-09/08/79 10,041 100 680 500 535 05/28/80-08/29/81 9.015 100 710 505 537 01 /05/82-08/12/83 10,680 100 685 501 536 07/24/84-11/30/85 9,040 98 690 502 536 03/04/86-08/08/88 10,305 100 710 505 536 11 /29/88-09/15/90 11,596 80 750 511 537 03/15/91-02107 /92 7,733 100

n/a

n/a 535 04/18/92-06/04/93 9.101 100 n/a n/a 533 11 /08/93-11130/94 6.533 100 n/a n/a 533 Cycles 9-11 steam generator data is not applicable due to steam generator replacement after Cycle 8.

(1)

On 04/19/77, T-ref was increased from 544 degrees to 549 degrees Fahrenheit.

(2)

On 11/07/77. 100% power was increased from 2212 MWth to 2530 MWth.

(1)

(2)

c v

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ATTACHMENT NO. 5 Consumers Power Company Palisades Plant Docket 50-255 RESPONSE TO NRC NOVEMBER 30,1994 REQUEST FOR ADDITIONAL INFORMATION REVISION 1 10CFR50.61 SCREENING CRITERION ITEM NO. 5 ABB-CENO RESPONSE

ABB - CENO RESPONSE All available purchase orders and receiving records were reviewed for shipments of weld wire W5214.

As shown in the attached table, four shipments of this material were received.

The approximate weight of each shipment is also tabulated. A total of 44,550 lbs of W5214 weld wire was received. Since this material was received in 150 pound spools, there were 297 spools. This data is summarized in Table 5-1.

The W5214 weld samples data base is given in Tables 5-2,5-3 and 5-4.

TABLE 5-1 W5214 Supplier Data P.O.#

Shipped Weight Coils (Calculated) 45-43953 7-23-65 7,200 48 45-43953 3-31-66 10,950 73 45-43953 6-24-66 io*.soo 72 45-43953 10-24-66 15,600 104 F* 1RVGIWP\\llA.l-QUES.WP

Table 5-2 Italicized Values are the Mean Value for one Weld Chemical Composition of Selected Heat No. W5214 Weld Samples Estimated Identification

%Cu

%Ni

%P Tandem No. of Location Arc Coils9.

04463 IP2 l-042B 0.20 0.019 x

8-12 Within weld; not first bead 04494 IP2 1-042 0.76 8-12 Through Thickness 0.77 0;72 0.81 0.96 0.98 0.98 1.01 0.99 0.97 0.96 1.05 1.08 0.81 1.01 1.06 1.03 1.03 1.00 0.81 0.94 04541 1.20 0.021 1

Weld Material Cert.

04577 IP2 0.94 0.02 8-12 Top 1 112" of weld L07 0.011 2 3/~6 from ID 1.00 0.02 04673 Millstone 1 1.05 5-7 Not determined; chip from weld SeamC 04674 IP2 3-042B 1.121 8-10 Not determined; chip from weld

Estimated Identification

%Cu

%Ni

%P Tandem No. of Location Arc Coils9 D4686 MLl 2-0.97 8-10 Weld chip 072A D4687 IP2 l-042A 0.92 8-12 Chip from Weld D4688 PAL SIG 0.99 3-5 Chip from Weld 5-943 D4690 1.13 o.02i 1-2 Test plate 1

D4691 o.02i WMC for Linde 80 D4752 0.0281 1-2 Test plate for Linde 80 1

D4982 0.0181 WMC for Linde 80 HBR2 torus-flange 4 Locations around the flange weld 0.154 0.99 0.012 OD surface8 0.163 0.90 0.011 0.152 1.08 0.014 0.166 1.002 0.012 0.159 0.99 0.012 x

10-12 IP2 Surveillance Weld 0.233 1.023 Charpy specimen W-13 7

0.203 1.063 Charpy specimen W-127 0.203 0.025 7

Tensile specimen W-6 7

1.003 Tensile specimen W-4 7

0.193 0.0107 Charpy specimen W-17 7

0.223 0.0177 Charpy specimen W-19 7

0.183 0.0227 Tensile specimen W-5 7

0.203 Tensile specimen W-37 o.2if J.OJ3 x

8-12 All test specimens were machined at locations through the weld 11 IP3 Surveillance Weld 0.15 1.02 0.019 Heat analysis 7

0.166 1.21 4

Charpy specimen W-15 7

0.158 1.12 0.019 x

2

Estimated Identification

% Cu

%Ni

%P Tandem No. of Location Arc Coils9 IP3 Nozzle cutout 0.16 1.06 0.017 x

Outside surface, 3/4 thickness, 0.15 1.11 0.018 center of weld8 0.15 1.09 0.018 0.15 1.09 0.018 8-12 HBR2 Surveillance Weld 0.32 0.66 0.021 Heat analysis 7 0.34 Heat analysis7 0.33 0.63 0.026 Charpy specimen W-17 0.35 0.695 Charpy specimen W-207 0.335 0.66 0.024 1

Oyster Creek 1 Surveillance Weld 0.282 0.0547"10 0.021 Charpy specimen 1E2A7 0.290 0.0567*10 0.023 Charpy specimen 1E2B7 0.2826 0.0517010 0.022 Charpy specimen 1E3 7 0.285 o.o5i*10 0.022 1

1Byrne (ABB/CE) to Kneeland (CPCo), "Records Search on Welds 2-112 A/C, 3-112 A/C, E-112 A/C, 9-112, Final Letter Report," P-MECH-92-025, October 12, 1992, Pg. 5-6.

2Yanichko, Williams and Kunka, "Evaluation of H.B. Robinson Unit 2 Reactor Vessel Beltline Region Weld Material Chemistry," May 1983, Table 4.

3Iddings, Cadena and Williams; "Reactor Vessel Material Surveillance Program for Indian Point Unit No. 2, Analysis of Capsule V," SWRI Project No. 17-2106 (Revised), March 1990, pg. IV-26.

4Y anichko, Anderson and Kaiser, "Analysis of Caps~le Y from the Power Authority of the State of New York Indian Point Unit 3 Reactor Vessel Radiation Surveillance Program," WCAP-10300, March 1983, pg. 4-3.

5Yanichko, Williams and Kunka, "Evaluation of H.B. Robinson Unit 2 Reactor Vessel Beltline Region Weld Material Chemistry," May 1983, Table 1.

6Chen (GPUN) to Kneeland (CPCo), November 4, 1992, pg. 5.

70akridge PR-EDB Version 2 8Evaluation of H.B. Robinson Unit 2 Reactor Vessel Beltline Region Weld Material Chemistry dated 5/83.

9Best Estimate by ABB CE.

10Nickel content for information only; not a nickel addition weld.

11Telecon, James F. Williams, Westinghouse Science and Technology, December 2, 1994.

ATTACHMENT TO TABLE 5-2 WELD WIRE HEAT W5214 COPPER SAMPLE DATA SET DESCRIPTION

1. D4463 IP-2 Weld l-042B Source:

In-process sample chipped from longitudinal weld seam fabricated by tandem arc weld process. Precise location unknown.

Application:

Value is not considered independent of IP-2 surveillance weld copper samples and is averaged in with the surveillance data.

Estimated No. of Coils:

8 to 12 coils

2. HBR2 Torus - Flange Weld Source:

Four samples cut from weld surface at four points around circumference of reactor vessel head. The four points represent approximately the same layer because the tandem arc welding most likely used the same pair of coils at each location.

Applica~ion: Four values are not considered independent of each other, and therefore are averaged and weighted by two coils (tandem arc weld).

Estimated No. of Coils:

10 to 12 coils

3. IP-2 Surveillance Weld

Note:

Source:

Eight Charpy and tensile specimens from the two surveillance capsules were analyzed for copper content. The specimens were removed from the outer 9-10 inches of a 11.75 inch thick weld. Individual specimen locations were provided by Westinghouse (James F. Williams and Richard Rishel, Westinghouse Science and Technology, December 21, 1994) The weldment was a prolongation (i.e., an extension) of one of the welds 1-042, A, B and C which were deposited using the tandem arc process.

Application:

The test specimens represent three unique weld wire coil combinations through the weld as follows:

Region #1, 1 to 5-1/2 inches Spec. No. Wl9, W3, W4*, W5 and W6 and D4463 Average Copper = 0.20%

Copper of 0.12 % was measured for specimen W4 but was excluded from average.

Re"gion #2, 5-1/2 to 7 inches Spec. No. W12 and W13 Average Copper = 0.215%

Region #3, 8 to 9 inches Spec. No. Wl 7 Average Copper = 0.19%

The three independent averages are weighted by two coils (tandem arc weld).

Estimated No. of coils:

8 to 12 coils

4. IP-3 Surveillance Weld Source:

Two test results were obtained. The first was an analysis of a sample from the surveillance weldment. The second was an analysis from an irradiated Charpy specimen. The two results are likely to be from two separate locations in the full thickness weldment which was deposited by the tandem arc process.

Application: The test results are likely to be independent, but are likely to represent as few as one unique weld wire coil combination. Therefore, the values were averaged and weighted by two coils (tandem arc weld).

Estimated No. of coils:

2 coils

5. IP-3 Nozzle Cutout Source:

A section of the IP-3 upper shell course longitudinal weld seam was contained in a nozzle dropout. The weld was analyzed by Westinghouse at three through-thickness locations: outside surface, 3/4 thickness, and weld center. The weld was deposited using the tandem arc process and was produced separately from the IP-3 surveillance weld.

Application: The three analyses represent unique locations through the weld thickness. The analyses represent three independent locations through a volume which would have required approximately three separate welding sequences (i.e., one sequence is movement of welding machine from seam A to B to C). Therefore, the three measurements are from three unique weld wire coil combinations and are weighted by two coils (tandem arc weld).

Estimated No. of coils:

8 to 12 coils

6. HBR-2 Surveillance* Weld*

Source:

Four analysis results were obtained. Two represent a sample from the surveillance weld and two represent individual Charpy specimens.

Specific locations of the four results were not determined because the weld is reported to have been fabricated by the single arc process using a single coil of weld wire.

Application:

Because the weld process was single arc and used a single coil, the four copper values were averaged and weighted by one coil (single arc, single coil).

Estimated No. of coils:

1 coil

7. Oyster Creek Surveillance Weld Source:

Three analysis results were obtained from three Charpy specimen samples. Specific locations of the three samples has not been determined. The surveillance weld was fabricated by the single arc process without any nickel addition.

Application:

Because the weld was fabricated by the single arc process and is estimated to have used a single coil of weld wire, the three copper values were averaged and weighted by one coil (single arc, single coil).

Estimated No. of Coils:

1 coil

8. Palisades Steam Generator Welds Source:

Nine samples were obtained from three depths (through thickness) from the three axial welds (i.e., three samples from each of the three welds) of the Palisades steam generator No. 1. The three welds were fabricated

together using a tandem arc process, following the same sequence for each given level in each weld. The samples were taken at 0.95 inches (sample x), 2.9 inches (sample Y), and 3.8 inches (sample Z) from the weld inside surface.

Application:

Three separate regions were identified based on level obtained (x, y or z) and the consistency of the copper measurements as follows:

Region 1, All X - level results SeamC Seam A SeamB

.336 Cu

.364

~

.348 avg.

Region 2, Two Y - level results and two Z - level results Seam C, Level Y Seam C, Level Z Seam A, Level Y Seam A, Level Z

.294 Cu

.260

.296

~

.277 avg.

Region 3, Remaining Y - level and Z - level results Seam B, Level Y Seam B, Level Z

.224 Cu

..m._

.226 avg.

The X-level results are clearly grouped based on copper content consistency and weld sequence (i.e., the inside weld at the X-level would have followed the same sequence for all three axial welds). The Y and Z - level results were grouped as given above based on consistency of results and the observation that the seam B weld location was likely to have been completed in one sequence of welding. The average values were weighted by two coils, giving a total of 3 measurements X two coils = 6 values consistent with the total of six unique coils.

Estimated No. of coils:

6 coils

TABLE 5-3 RESULTS OF CHEMICAL TESTING ON PALISADES RETIRED STEAM GENERATOR WELD MATERIAL Mn Cr Cu Mo Ni p

Si s

v

of Location coils Section through large Weldment 'A' ARl/X 1.179 0.0376 0.328 0.508 1.116 0.008 0.267 0.0128 0.0021 6

24 mm from ID ARl/Y 1.259 0.0349 0.310 0.515 1.006 0.007 0.256 0.0169 0.0021 48 mm from OD ARl/Z 1.205 0.0343 0.266 0.509 1.104 0.009 0.267 0.0181 0.0020 24mm from OD Section through large Weldment 'B' BRl/X 1.270 0.0415 0.198 0.552 1.092 0.013 0.177 0.0150 0.0026 6

24 mm from ID BRl/Y 1.308 0.0398 0.198 0.545 0.906 0.011 0.174 0.0150 0.0026 48 mm from OD BRl/z 1.283 0.0395 0.196 0.547 1.057 0.010 0.177 0.0157 0.0026 24 mm from OD Section through Trepan

'A/SG/A' A/SG/A/3/X 1.142 0.0407 0.365 0.510 1.193 0.006 0.241 0.0092 0.0020 6

24 mm from ID A/SG/A/3/Y 1.118 0.0343 0.292 0.501 1.127 0.009 0.277 0.0163 0.0018 48 mm from OD A/SG/A/3/Z 1.116 0.0334 0.281 0.500 1.066 0.011 0.274 0.0176 0.0019 24 mm from OD Section through Trepant

'A/SG/B' A/SG/B/2/X 1.177 0.0409 0.359 0.515 1.204 0.007 0.251 0.0111 0.0019 6

24 mm from ID A/SG/B/2/Y 1.120 0.0397 0.239 0.524 0.960 0.007 0.286 0.0131 0.0020 48 mm from OD A/SG/B/2/Z 1.092 0.0390 0.228 0.516 1.107 0.006 0.278 0.0138 0.0020 24 mm from OD Section through Trepan

'B/SG/A' B/SG/A/3/X 1.259 0.0394 0.191 0.535 1.256 0.010 0.176 0.0140 0.0023 6

24 mm from ID B/SG/A/3/Y 1.226 0.0375 0.192 0.537 1.292 0.011 0.190 0.0149 0.0024 48 mm from OD B/SG/A/3/Z 1.220 0.0378 0.204 0.531 0.998 0.011 0.198 0.0166 0.0024 24 mm from OD Section through Trepan

'B/SG/B' B/SG/B/3/X 1.269 0.0395 0.165 0.534 1.117 0.009 0.183 0.0136 0.0024 6

24 mm from ID B/SG/B/3/Y 1.241 0.0393 0.203 0.524 1.088 0.007 0.190 0.0139 0.0023 48 mm from OD B/SGB/3/Z 1.183 0.0388 0.209 0.526 1.292 0.008 0.210 0.0129 0.0025 24 mm from OD Rows beginning with "A" are Heat No. W5214.

Rows beginning with "B" are Heat No. 34B009.

TABLE 5-3 (continued)

Mn Cr Cu Mo Ni p

Si s

v

of Location coils Section through large Weldment 'A' Al/l/X 1.157 0.0371 0.341 0.502 1.093 0.010 0.264 0.0146 0.0023 6

24 mm from ID Al/l/Y 1.249 0.0339 0.310 0.507 1.003 0.010 0.265 0.0174 0.0022 48 mm from OD Al/l/Z 1.176 0.0317 0.266 0.487 1.090 0.011 0.288 0.0181 0.0022 24 mm from OD Section through large Weldment 'B' Bl/2/X 1.249 0.0400 0.235 0.546 1.215 0.012 0.173 0.0159 0.0028 6

24 mm from ID Bl/2/Y 1.304 0.0383 0.189 0.537 1.010 0.012 0.166 0.0182 0.0028 48 mm from OD Bl/2/Z 1.265 0.0389 0.196 0.540 1.098 0.012 0.182 0.0177 0.0028 24 mm from OD Section through Trepan

'A/SG/A' A/SG/A/2/X 1.137 0.0401 0.367 0.508 1.154 0.011 0.247 0.0115 0.0021 6

24 mm from ID A/SG/A/2/Y 1.120 0.0328 0.291 0.498 1.156 0.013 0.284 0.0178 0.0020 48 mm from OD A/SG/A/2/Z 1.114 0.0333 0.278 0.498 1.059 0.012 0.284 0.0182 0.0021 24mm from OD Section through Trepant

'A/SG/B' A/SG/B/3/X 1.173 0.0407 0.353 0.515 1.203 0.011 0.243 0.0110 0.0021 6

24 mm from ID A/SG/B/3/Y i.102 0.0389 0.233 0.523 1.149 0.012 0.291 0.0158 0.0024 48 mm from OD A/SG/B/3/Z 1.105 0.0411 0.237 0.519 1.024 0.011 0.302 0.0141 0.0025 24 mm from OD Section through Trepan

'B/SG/A' B/SG/A/2/X 1.292 0.0412 0.195 0.551 1.272 0.017 0.186 0.0181 0.0031 6

24 mm from ID B/SG/A/2/Y 1.234 0.0379 0.195 0.550 1.331 0.016 0.202 0.0170 0.0027 48 mm from OD B/SG/A/2/Z 1.246 0.0388 0.206 0.544 1.138 0.016 0.211 0.0165 0.0027 24 mm from OD Section* through Trepan

'B/SG/B' B/SG/B/2/X 1.273 0.0397 0.162 0.541 1.126 0.016 0.191 0.0177 0.0029 6

24 mm from ID B/SG/B/2/Y 1.237 0.0402 0.208 0.536 1.136 0.016 0.204 0.0165 0.0027 48 mm from OD B/SG/3/2/Z 1.188 0.0391 0.209 0.532 1.307 0.016 0.212 0.0156 0.0025 24 mm from OD Rows beginning with "A" are Heat No. W5214.

Rows beginning with "B" are Heat No. 34B009.

Table 5-4 Chemical Analyses of Palisades Weld Seams Wetd Sample Analysis Copper Nickel Section Location Method (wt%)

(wt%)

A1/1 x

AEA-1 0.341 1.093 AEA-2

. 0.328 1.116 ICP 0.345 0.831 OES 0.33 1.09 AVERAGE 0.336 1.03 A1/1 y

AEA-1 0.310 1.003 AEA-2 0.310 1.006 ICP 0.256 1.101 OES 0.30 1.05 AVERAGE 0.294 1.04 A1/1 z

AEA-1 0.266 1.090 AEA-2 0.266 1.104 ICP 0.260 1.093 OES 0.25 1.10 AVERAGE 0.260 1.10 NSG/N2 x

AEA-1 0.367 1.154 AEA-2 0.365 1.193 ICP 0.350 1.232 OES+15 0.37 1.23 OES+35 0.37 1.29 AVERAGE 0.364 1.22 NSG/N2 y

AEA-1 0.291 1.156 AEA-2 0.292 1.127 ICP 0.310 0.983 OES 0.29 1.18 AVERAGE 0.296 1.11 NSG/N2 z

AEA-1 0.278

. 1.059 AEA-2 0.281 1.066 ICP 0.206 1.031 OES 0.27 1.16 AVERAGE 0.259 1.08 Page 1 of 3

Table 5-4 (Continued)

Chemical Analyses of Palisades Weld Seams We1d Sample Analysis Copper Nickel Section Location Method (wt%)

(wt%)

NSG/B/3 x

AEA-1 0.353 1.203 AEA-2 0.359 1.204 ICP 0.322 1.040 OES+17 0.34 1.15 OES+36 0.35 1.29 AVERAGE 0.345 1.18 NSG/B/3 y

AEA-1 0.233 1.149 AEA-2 0.239 0.960 ICP 0.202 1.*051 OES 0;22 1.22 AVERAGE

0.224 1.09 A/SG/B/3 z

AEA-1 0.237 1.024 AEA-2 o.228 1.107 ICP 0.228 1.002 OES-34 0.22 1.18 OES-10 0.22 1.11

.. AVERAGE 0.227 1.08 Page 2 of 3

Table 5-4 (continued)

Chemical Analyses of Palisades Weld Seams Weld Sample -Analysis Mn Cr Mo p

Si s

v Section Location Method-(wt%)

(wt%)

A1/1 x

AEA-1 1.157 0.0371 0.502 0.010 0.264 0.0146 0.0023 AEA-2 1.179 0.0376 0.508 Q.008 0.267 0.0128 0.0021 ICP 1.1682 0.0379 0.5171 0.0216 0.4017 0.0025 OES 1.18 0.05 0.50 0.011 0.26 0.011 0.002 A1/1 y

AEA-1 1.249 0.0339 0.507 0.010 0.265 0.0174 0.0022 AEA-2 1.259 0.0349 0.515 0.007 0.256 0.0169 0.0021 ICP 1.1537 0.0282 0.4665 0.0205 0.3441 0.0020 OES 1.29 0.04 0.51 0.013 0.26 0.014 0.002 A1/1 z

AEA-1 1.176 0.0317 0.487 0.011 0.288 0.0181 0.0022 AEA-2 1.205 0.0343 0.509 0.009 0.267 0.0181 0.0020 ICP 1.0969 0.0286 0.4740 0.0214 0.3824

<0.0005 OES 1.20 0.04 0.48 0.012 0.28 0.015 0.002 NSG/N2 x

AEA-1 1.137 0.0401 0.508 0.011 0.247 0.0115 0.0021 AEA-2 1.142 0.0407 0.510 0.006 0.241 0.0092 0.0020 ICP 1.0653 0.0397 0.4866 0.0325 0.3577

<0.005 OES+15 1.17 0.05 0.51 0.011 0.25 0.008 0.002 OES+35 1.20

. 0.05 0.51 0.011 0.24 0.009 0.002 A/SG/A/2 y

AEA-1 1.120 0.0328 0.498 0.013 0.284 0.0178 0.0020 AEA-2 1.118 0.0343 0.501 0.009 0.277 0.0163 0.0018 ICP 1.1448 0.0376 0.4835 0.0212 0.3466 0.001 OES 1.13 0.04 0.50 0.013 0.29 0.014 0.002 NSG/N2 z

AEA-1 1.114 0.0333 0.498 0.012 0.284 0.0182 0.0021 AEA-2 1.116 0.0334 0.500 0.011 0.274 0.0176 0.0019 ICP 1.0632 0.027 0.4692 0.0220 0.3662 0.007 OES 1.12 0.04 0.50 0.013 0.28 0.014 0.002 NSG/8/3 x

AEA-1 1.173 0.0407 0.515 0.011 0.243 0.0110 0.0021 AEA-2 1.177 0.0409 0.515 0.007 0.251 0.0111 0.0019 ICP 1.1543 0.036 0.4960 0.0218 0.3204 0.0022 OES+17 1.21 0.05 0.51 0.011 0.23 0.008 0.002 OES+36 1.16 0.05 0.50 0.011 0.24 0.009.

0.002 A/SG/8/3 y

AEA-1 1.102 0.0389 0.523 0.012 0.291 0.0158 0.0024 AEA-2 1.120 0.0397 0.524 0.007 0.286 0.0131 0.0020

ICP 1.1631 0.0372 0.5012 0.0236 0.3263

<0.0005 OES 1.12 0.05 0.52 0.012 0.29 0.011 0.002 NSG/8/3 z

AEA-1 1.105 0.0411 0.519 0.011 0.302 0.0141 0.0025 AEA-2 1.092 0.0390 0.516 0.006 0.278 0.0138 0.002 ICP 1.1062 0.0379 0.5233 0.0267 0.4127 0.0008 OES-34 1.14 0.05 0.52 0.012 0.29 0.012 0.002 OES-10 1.15 0.05 0.52 0.011 0.29 0.012 0.002 Page 3 of 3

WELD WIRE HEAT W5214 COPPER CONTENT MODEL EVOLUTION The physical basis for developing a best estimate copper for a heat of submerged arc weld wire must reflect the welding process, welding sequence, and the copper coating procel)s. The following describes the evolution of the model and summarizes the process information upon which the best estimate copper was based.

1.

Model Evolution - In November 1994, data from the Palisades retired steam generator welds was added to an existing set of weld deposit copper content data traceable to weld wire heat W5214. The premise at that point was that copper differences were a function of coil-to-coil variability in copper coating thickness. Therefore, a single arc weld sample would reflect the contribution from one coil, and a tandem arc weld sample would reflect two coils. Therefore, the copper data from a unique tandem arc weldment would be averaged and then weighted by two; copper data from a unique single arc weldment would be averaged and then weighted by one.

The three steam generator welds were used to generate three samples from specific levels through the weld for a total of nine samples. The primary question was how to treat those nine results in conjunction with the original data base. The use of nine tandem arc samples from the generator welds (i.e., eighteen values) would clearly bias the calculation of a best estimate for a W5214 weldment. The use of an average from each of the three generator welds implies that each seam was unique, which in fact is not the case. (See process discussion which follows.) Therefore, the nine sets of copper values were averaged together and weighted as one tandem arc w~ld which was consistent with the fact the three welds were produced sequentially.

An assessment was made of the nine steam generator weld data to determine how many unique copper values were represented. Three unique sets were identified based on relative level in the weld, variation in measured copper, and welding sequence. The three average copper values, therefore, represent the deposition of three unique weld

wire combinations; i.e., a series of weld beads which were deposited using the same two coils by a tandem arc process. However, the basis for the original data set was different. It represented a bulk weld value of copper without full consideration for the number of unique weld wire coil combinations used to fabricate each bulk weld.

In order to put the steam generator data on the same basis as the original data, the latter were considered two different ways. The initial approach was to take each original measurement (but not averaged) and weight it using the single or tandem arc concept.

This approach, however, has little direct relation to the total number of weld wire coil combinations being samJ:Jled. Therefore, the first approach was rejected. The next approach took the original data and described it on the basis of unique weld wire coil combinations together with the single or tandem arc weighting concept. The concept was to determine the specific location of each original chemical analysis sample, similar to what was done for the steam generator data, and provide subsets of unique weld wire coil combinations. A total of 13 unique weld wire coil combinations were identified, including the three steam generator weld wire coil combinations, yielding a

_weighted set of 24 copper values. This approach enabled the evaluation to proceed on the same basis (i.e., weld wire coil combinations), thereby describing coil-to-coil copper variability more precisely.

2.

Welding Process - Automatic submerged arc welding using wire heat W5214 is summarized below:

a)

Single Arc - In this process, a single coil of wire was fed through the welding head at a specified feed rate. The welding head progressed at a specified travel speed along the length of a longitudinal seam and around the circumference of a girth weld. A single weld bead was deposited at one depth in the weld.

Multiple passes produced successive layers of weld beads.

b)

Tandem Arc - In this process, two coils of wire were fed through the weld heads, one leading and one trailing head. The process is otherwise the same as the single arc process, except that tandem arc welding had a higher deposition rate and was typically used for longitudinal seams.

c)

Nickel Addition - Both single arc and tandem arc welding could be performed with a nickel addition. The submerged arc (i.e., W5214) wire was melted by the arc whereas the nickel was fed in "cold" and was melted in the weld puddle.

The nickel feed rate was controlled resulting in a specified percentage of nickel in the weld deposit (typically 1 %).

3.

Welding Sequence Longitudinal welds were produced following a specific sequence which include all the seams in a given shell course as shown in Figure 1. Reactor vessel and steam generator shell weld joints were in a "double U" configuration as shown in Figure 2.

The welding sequence is depicted in Figure 3 for the retired Palisades steam generator upper shell longitudinal welds (from which the chemistry samples were extracted).

Thicker welds, such as for reactor pressure vessel longitudinal seams, are similar except that additional sequence steps are performed.

The welding sequence is designed to retain dimensional control of the shell. If it were not done in steps from seam to seam, the thermal stresses from welding could

. permanently distort the shell. The initial weld passes start at the outer weld root, as shown in Figure 3. The outer weld root is partially filled. for each seam in series.

Once all three seams are partially filled, the weld root is mechanically removed, including most of the machined extension of adjoining plates plus some of the first pass weld in the outer root. The inner root of seams A and B is then welded to a partial depth, and then the inner root of seam C is completely filled. The welding machine is then repositioned to complete seams A and B to the inside surface. The final sequence

is to complete seams A, B, and C in series to the outer surface. (For thicker welds, the outer welds are typically performed in three separate sequences).

Girth welds were typically produced using a straight sided weld. Welding started at the inSide surface and progressed through the weld to the outside surface. A single weld bead would be deposited around the circumference at a single depth in the weld.

For both longitudinal and girth welds, the width of the weld would be comprised of several weld beads. A typical weld was three weld beads across the width.

4.

Copper Coating Process The submerged arc wire was coated with copper. It is a batch process such that multiple coils were dipped in the bath at one time. For the approximately 300 coils obtained for heat W5214, as many as 30 separate batches could be represented.

Combustion Engineering's purchase specification for the W5214 wire stipulated a maximum of 0.20% copper in a resultant weld deposit. Therefore, it is expected that the supplier instituted process controls for copper coating which were intended to comply with the purchase specification. This in turn implies that the majority of the batches of coils would have met the. 0}0% copper limit. Therefore, the majority of welds fabricated using W5214 weld wire would also be expected to not exceed 0.20%

copper because the weld deposit copper content is a direct result of the copper from the weld wire.

I

' I

, -\\

I FIGURE 1 FITUP OF UPPER SHELL

~

I I

I,_

I

~ ',,,, -

... ~'

) I

-: ~

CIRCUMFERENTIAL DIRECTION IN VESSEL SHELL AXIAL DIRECTION IN VESSEL SHELL

FIGURE 2 SHELL FITUP - TOP VIEW

FIGURE 3 TYPICAL WELDING SEQUENCE 10 A

STEP 4 IS BACKGROOVE

Statistical Analysis of the Chemistry of Heat W5214 As described earlier, the welding process consists of running a bead down the weld groove, feeding weld material from orie or two 150 pound coils. Because the coils are dipped into the coating bath in batches, the variation in copper content from coil to coil accounts for most of the spread in observations of weld copper content. This is supported by the chemical analysis results which showed consistent Cu content within the weld deposit from one weld wire coil combinations.Discontinuities in copper content are believed to be caused by different weld wire coil combinations. Also the B&W weld studies1 showed very little variation in copper content along bead length.

Table 5-5 summarizes the. samples of W5214 selected for weld wire coil combinations independence and gives the measured copper content of the samples. Also shown is the type of weld process (single or tandem) and description summary. The basis for the sample selection was the independence of the weld material.

Multiple readings of the same weld wire coil combinations were averaged to be a single reading when their inclusion as multiple independent samples would bias the results to that specific weld wire coil combination.

Item 8 of the attachment to Table 5~2 gives the three weld regions from the Palisades steam generator. These weld regions are discussed in the response to RAI Item 6.

The selection of the independent samples was performed in a two step Delphi Technique2* In the first step, weld and material experts from ABB-CE reviewed the data presented in Table 5-2 and selected independent samples. On 12/20/94, a larger group of expertS, including people working on the reactor vessel integrity for six different companies met to review the method and data selection.

The attendance list is given as Table 5-6.

Starting with the original ABB-CE screening, the group reviewed all the data given in Table 5-2, and supporting information. They reached a consensus that the data given in Table 5-5 is the most likely representation of separate weld wire coil combinations for heat W5214.

Because tandem welds are a combination of two weld coils, the tandem welds are given a weight of two. Table 5-7 gives the weighting of each sample. Table 5-7 also gives the median, mean

and cumulative probability distribution that the copper content of a weld is less than or equal to a specific percent (X).

The best estimate as suggested by 10CFR50.61 is the mean value. If the mean is used, the best estimate of the copper content of the Palisades reactor vessel (beat W5214) is 0.212% Cu. The mean credits the lower frequency, higher Cu content data; therefore, it is conservative. It has a 653 probability quantile on the cumulative probability distribution. That means, on average, a 65 3 chance that the welds will have less copper than the mean. The median for these samples is 0.193 Cu. There is a 503 probability that the welds will have either a higher or lower content than the median value of 0.193 Cu.

Figure 5-4 gives the frequency distribution of the samples. The distribution peaks at the low copper content and trails off as Cu 3 increases. It is not a normal distribution and the one sigma value has no meaning.

The phosphorus content of heat W5214 is estimated in Table 5-8. The data for the specific samples is from Tables 5-2 and 5-4 and is grouped in the same manner as the copper content data. The additional samples for which P content was available but Cu content was unknown has been added.

The best estimate <mean) Phosphorus content for heat W5214 is estimated as 0.017%.

1.

Moore, K., B&W NT, Personal Communication, December 20, 1994.

2.

Gautschi, T.F., "Group Decision Making," Design News, April 4, 1983, Page 122.

TABLES-5 WELD BEAD SAMPLES USED FOR CHARACTERIZATION OF HEAT W5214 SAMPLE!

CU%

ITIE DESCRIPTION

SUMMARY

IP3 NOZZLE CUTOUT 0.15 TANDEM Three different depths IP3 NOZZLE CUTOUT 0.15 TANDEM Three different depths IP3 SURV 0.158 TANDEM Avg of 2 readings HBR2,TORUS-FLANGE 0.159 TANDEM 4 readings, same depth IP3 NOZZLE CUTOUT 0.16 TANDEM Three different depths IP2 SURV, REGION 3 0.19 TANDEM 1 location IP2 SURV, REGION 1 0.20 TANDEM 4 close locations IP2 SURV, REGION 2 0.215 TANDEM 2 close locations PAL SG, REGION 3 0.226 TANDEM Same weld wire coil combination PAL SG, REGION 2 0.277 TANDEM Same weld wire coil combination OYSTER CREEK 1 SURV 0.285 SINGLE 3 readings, 1 coil HBR2 SURVEILLANCE 0.335 SINGLE 4 readings, 1 coil PAL SG, REGION 1 0.348 TANDEM Same weld wire coil combination

Samples ordered by increasing copper content.

TABLES-6 MEMBERS OF THE DELPffi TEAM* REVIEWING HEAT W5214 DATA NAME COMPANY D. Ayres ABB-CE J. Biffer CPCo S. Byrne ABB-CE J. Chapman YAEC V. Dimitrijevic YAEC B. Gerling CPCo C. Gimbrone ABB-CE R. Hardies BGE C. Hoffmann ABB-CE J. Kneeland CPCo P. Leombruni ABB-CE K. Moore B&WNT W. Server ATI E. Siegmann ABB-CE B. Woodman Packer

Meeting on 12/20/94, Windsor, CT

TABLES-7 PROBABILITY DISTRIBUTION FOR COPPER IN HEAT W5214 Analysis of Samples of Heat W5214 Sample Description Cu%

Weight Cu%* Wt.

P(CU:::; x)

IP3 NOZZLE CUTOUT 0.15 2

0.3 IP3 NOZZLE CUTOUT 0.15 2

0.3 0.167 IP3 SURV 0.158

.2 0.316 0.250 HBR2, TORUS-FLANGE 0.159 2

0.318 0.333 IP3 NOZZLE CUTOUT 0.16 2

0.32 0.417 IP2 SURV, REGION 3 0.19 2

0.38 0.500 MEDIAN 0.19 0.50 IP2 SURV, REGION 1 0.2 2

0.4 0.583 MEAN 0.212 0.65 IP2 SURV, REGION 2 0.215 2

0.43 0.667 PAL SG, Region 3 0.226 2

0.452 0.750 PAL SG, Region 2 0.277 2

0.554 0.833 OYSTER CREEK 1 SURV 0.285 1

0.285 0.875 HBR2 SURVEILLANCE 0.335 1

0.335 0.917 PAL SG, REGION 1 0.348 2

0.696 1.000 Sum=

24 5.086 MEAN 0.212 MEDIAN 0.19

TABLES-8

MEAN ESTWATION OF PHOSPHORUS CONTENT IN HEAT W5214 Best Estimate of Phosphorus in heat W5214 Sample Name

%P Weight

%P *Wt.

IP3 NOZZLE CUTOUT 0.017 2

0.034 IP3 NOZZLE CUTOUT 0.018 2

0.036 IP3 SURV 0.019 2

0.038 HBR2, TORUS-FLANGE 0.012 2

0.024 IP3 NOZZLE CUTOUT 0.018 2

0.036 IP2 SURV, REGION 3 0.01 2

0.02 IP2 SURV, REGION 1 0.021 2

0.042 IP2 SURV, REGION 2 N.A.

N.A.

PAL SG, REGION 3 0.0131 2

0.0262 OYSTER CREEK 1 SURV 0.022 1

0.022 PAL SG, REGION 2 0.0135 2

0.027 HBR2 SURVEILLANCE 0.024 1

0.024 PAL SG, REGION 1 0.0135 2

0.027 D4541 0.021 1

0.021 D4577 0.02 1

0.02 D4690 0.027 1

0.027 Mean=

0.017

FIGURE 5-4 *

HISTOGRAM OF COPPER CONTENT FOR HEAT W5214 11 10 I

8 U) w

...I 7 a..

IE 4C 6 U)

u.

0 6

0 z 4 3

2 1

0 0.140-0.179 0.180-0.219 0.220-0.269 0.260-0.299 0.300-0.339 0.340-0.379 X (24 DATA)

ATTACHMENT NO. 6 Consumers Power Company Pa~ i sades Pl ant Docket 50-255 RESPONSE TO NRC NOVEMBER 30,1994 REQUEST FOR ADDITIONAL INFORMATION REVISION 1 10CFR50.61 SCREENING CRITERION ITEM NO. 6 STATISTICAL EVALUATION OF COPPER CONTENT IN STEAM GENERATOR WELDS BY ABB - CENO

Statistical Evaluation of Copper Content In Steam Generator Welds An evaluation_ of the chemistry data developed on the Palisades retired steam generator welds, was undertaken to determine how the data should be combined with the existing data base on the weld material W5214. The analysis described below resulted in the conclusion that there are three distinct copper content regions in the tandem welds which are appropriate for inclusion in the data base for W5214.

The steam generator weld chemistry data was analyzed to evaluate the number of distinct weld regions resulting from usage of distinct weld wire pairs. This analysis employs a weld process

-based conclusion that the steam generator (SG) data represents samples from three distinct weld wire coil combinations. Based on knowledge of the weld process and the number of coils used, three distinct regions of weld wire coil combinations are expected.

The most straightforward assumption regarding a model for the SG data is that data taken from a given depth represents sampling from a unique weld wire coil combination. This being the case, the through thickness variability in the SG data is expected to be consistent with the through thickness variability in the remainder of the heat W5214 data set.

The F test was used to compare a pooled estimate of the variance for the SG data with an

estimate of the variance from the other W5214 data. 'The results of this statistical test are consistent with the hypothesis for analyzing the SG data set as three separate welds.

The Student's T test was used to evaluate the statistical significance of difference between the mean values of the SG data set and that of the other W5214 data. The difference in means was highly significant in the statistical sense. The conclusion from this portion of the analysis is that the total W5214 data set represents a complex statistical family of distributions in which the weld wire coil combination variability is dominant.

The SG data subset copper values are not out of the range of the other W5214 data as seen in Figure 5-5 in the response to RAI Item 5. The data is encompassed by the HBR-2

Surveillance and Oyster Creek-1 Surveillance results. The range of copper content seen in the overall data set is not inconsistent with that seen in other heats of weld material, e.g. NUREG CR6249, "Unirradiated Material Properties of Midland Weld WF-70," October 1994.

The results of this statistical evaluation assure that the steam generator weld provides independent data on three pairs of weld wire coil combinations and that each weld wire coil combination belongs to the same family of distributions as the prior data on W5214 pf Table 5.2. Therefore, the steam generator weld provides three data points with Cu contents of 0.348, 0.277, and 0.226 wt%, which are appropriate for inclusion in the set of data to describe the properties of weld heat W5214. The effect of the inclusion of this data is presented in the response to RAI Item 5.

ATTACHMENT NO. 7 Consumers Power Company Palisades Plant Docket 50-255 RESPONSE TO NRC NOVEMBER 30,1994 REQUEST FOR ADDITIONAL INFORMATION REVISION I 10CFR50.61 SCREENING CRITERION PLAN FOR ADDRESSING WELD MATERIAL TEST RESULTS I Page

PLAN FOR ADDRESSING WELD MATERIAL TEST RESULTS It is Consumers Power Company's intention to determine (1) if some type of phenomenon may have influenced the initial material properties of the Palisades steam generator welds and (2) if material properties can be restored sufficiently to allow for use of that weld material in the Palisades reactor vessel surveillance program for determining the response of the reactor vessel material to irradiation. The plan will evolve as we proceed, but is expected to follow this general scenario.

1.

Characterize the steam generator weld materials by investigating the spatial variation in bulk chemistry and material properties. Detailed composition maps of the copper and nickel levels are being prepared using X-ray microprobe.

A hardness survey will also be performed. This information is intended to aid in the selection of locations for test specimens.

2.

Perform a pilot heat treatment program for the purpose of determining the optimum heat treatment required to restore or approach the initial material properties. The program will concentrate on recovery of the upper shelf energy and tensile and hardness properties.

3.

Perform heat treatment on a full complem~nt of test specimens to determine the amount of recovery of the mechanical properties.

4.

Perform microstructural examination of the "aged" and "regenerated" weld materials for the purpose of determining the soluble copper content, and hence, its expected response to irradiation will be representative. This will be established by microstructure examination of a comparison weld or welds, which is also planned.

Potential candidates include the Palisades surveillance weld or surveillance material from H. B. Robinson 2, Indian Point 2 or Indian Point 3.

Completion of this program by March 1, 1995 is essential for addressing the future of the supplemental surveillance program, still planned for implementation during the 1995 refueling outage.

v t e Letter Sequence Response to RAI
TAC:M83227, (Approved, Closed)
Initiation Request Acceptance... Administration Questions 30 November 1994 Answers 28 December 1994 Results Approval, Approval, Approval Other: ML18059B177, ML18064A576
MONTHYEAR1994-07-12 [Table View]

ML18064A533

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