ML17251A481

Ultrasonic Indication Sizing Technique Development. Related Info Encl

ML17251A481
Person / Time
Site:	Point Beach, Ginna, 05000000
Issue date:	02/28/1989
From:	SOUTHWEST RESEARCH INSTITUTE
To:
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ML17251A482	List: ML17251A481 ML17309A425
References
NUDOCS 8905160235
Download: ML17251A481 (64)

Text

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ULTEMSONICINDICATIONSIZING TECHNIQUE DEVELOPMENT DRAFTFINALEXPORT SwRI Project 2388 Prepared for Rochester Gas & Electric Corporation 89 East Avenue Rochester, New York 14649 Wisconsin Electric Power Company 6610 Nuclear Road Two Rivers, Wisconsin 54241 Prepared by Nondestructive Evaluation Science and Technology Division February 1989 S 9Og pg~Sl6Opp~

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TABLEOF CONIEKlS L

INTRODUCIION o

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1 II BACKGROUND....

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4 IIL TECHNICALDISCUSSION A.

Introduction B.

Inspection Techniques..

G Test MOCRUps

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D.

Technique Evaluation..

E.

Pmaxfure Development F.

Evaluation of the Framatome Focused Scarce U CBl441 UQlts

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9 11 11 12 V.

CONCLUSIONS................

13 A

Welding Flaw's in Reactor Pressure Vessel Nozzle-to-Shell Welds B

Focused-Beam Sizing Data C

Timewf-Flight Sizing Data

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I. INTRODUCIION Ultrasonic examinations to locate and size Qaws in the nozzle-to-shell welds in reactor pressure vessels (RPV) have long been performed by positioning the transducers on the inner bore of the nozzles.

These examinations have been very satisfactoty for detecting Qaws and for locating small fabrication-induced indications parallel to the fusion line of the weld. Some problems have becom apparent, however, when attempting to size the Qaws using transducers simQar to those applied for detection.

Problems include the inability to locate the end points in both the circumferential and through-wall (axial) directions accurately enough to estimate, respectively, the length and depth of planar Qaws in the weld. It is believed that the cylindrical or in some cases conical bores of the nozzles distort the beam, which complicates accurate sizing. One technique for sizing Qaws in the nozzle-bore region has been to perform a type of beam focusing by removing the transducer beam spread from the actual sizing measurement.

The intent has been to attain a more conservative and accurate flaw length and depth estimate.

Beam-spread sizing techniques have been used since 1976 to size Qaws during nozzlekore examina-tions at both the Point Beach and R. E. Ginna nuclear plants. While this approach was considered

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adequate, it was recognized that several recently developed and weH documented Qaw-sizing techniques had proven to be quite accurate in various tests such as the PISC trials. These tech-niques also had been applied successfully in other types of field examinations.

Because of the availability of the new Qaw-sizing techniques, a project was initiated at Southwest Research Institute (SwRI) in August 1988 by Wisconsin Electric Power Company and Rochester Gas 4 Electric Corporation to evaluate two ofthese techniques.

The purpose was to develop their applicability for addressing the nozzlekore Qaw-sizing problems encountered at Point Beach and R. E. Ginna. The project consisted ofbuilding mockups ofthe speciQc geometries involved, placing planar reQectors at the location of the fusion line of the nozzle-to-vessel welds (where indications

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lylocated), and performing Qaw-sizing exercises withnew y p

newl develo ed transducer-technique combinations to prove the adequacy of the selecte pp d a roaches.

Finally, the Qaw-sizing data a uired from data acquire usmg e new proc d 'h ocedures was to be compared with Qaw-sizing cq

'erforming conven 'on exai

'i al exaininations on the nozzle mockups following p

ASME Code rocedures (see Figure I).:Ihe two special procedures chosen for this prospect used ( )

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(I) lar diameter focused transducers with amplitudeArop sizing techniques (Figure 2) and (2) conventional transducers wi timewf-Qight techniques for detecting the difKracted signals from th rp the sha ends of the planar Qaws in both the through-wall (depth) and circumferential (length) directions (Figure 3).

Figure I. Straight%earn, unfocused. transducer approach (Code<izing technology)

Figure 2. Straight-beam, focused transducer approach (focused-beam technology)

Figure 3. Angle-beam, unfocused transducer approach (timewf-Qight technology)

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IL BACKGROUND The transducer-technique combinations chosen forevaluation have been well documented in recent studies by the Electric Power Research Institute and other organizations engaged in ultrasonic examination research and development.

The f tec has been used for a number of years by an examination agency in France to size small Qaws in the nozzle-to-shell weld region as well as elsewhere in the reactor vessel walL Variations of the ti elf-i ht techno o have been applied by a number of agencies in Europe, the Orient, and the United States.

SwRI has a signiGcant amount of experience in timewf-Qight Qaw identification and sizing techniques, many of which have been developed by Dr. George J. Gruber.

IIL TECHNICALDISCUSSION A. Introduction The scope of this project was to develop Qaw-sizing techniques to be used in the two nozzle conGgurations present in the Point Beach and R. E. Ginna RPVs.

One mockup conGguration simulated the inlet/outlet nozzles; the other the core-Qood, or safety-injection, nozzles. The inlet/

outlet nozzle, with a conical bore diameter of approximately 30 inches, was cladded with stainless steel and then hand ground to a relatively smooth Qnish.

The core-Qood nozzle, with a 3.4-inch diameter bore, was also cladded with stainless steel, but was machined smooth.

These two geom-etries represented signi6cantly different problems that had to be addressed in order to direct and

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control the ultrasonic beams at the areas of interest.

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B. Inspection Techniques The focused-beam Qaw-sizing technology employed largeMiameter transducers to focus the ultrasonic beam to as small a point as practical at the specific depth locations of the reQectors.

The focused beam was moved across each reQector utilizingan amplitud~p technique to deGne the reQector edges.

Because the beam diameter at the reQector location was small relative to the size of each reQector, the ability to accurately deGne and locate the edges of the reQector was signiQcantly enhanced.

To do this, the bore configuration ofboth nozzles had to be carefully taken into consideration in the design of the transducer lenses so that proper focusing could take place in the materiaL An additional consideration was the plane of the reflector, which is typically oriented several degrees offnormal from the nozzle bore.

Once the lens was designed, it was just as important to assure that the mechanical scanning equipment could position the transducer accurately relative to the bore of the nozzle so that the sound beam was focused properly in the test materiaL The timewf-Qight flaw-sizing technology was based upon the selection of conventional trans-ducers; no attempt was made to focus the ultrasonic beam.

The approach was to introduce the sound beam obliquely to the reQector so that the strong specularly reQected waves-which can mask the real ti~iQracted waves-were not returned to the transducer.

This approach allowed observance of the diffracted signals f'rom all four edges of a planar reQector.

Accurate screen-distance calibration permitted the measurement of the times that it took for a pair of diffracted signals (doublet) to reach an axially (or circumferentially) scanned transducer.

Simple ray-tracing calculations were performed that considered the sound-beam angle and the relationship between the difference intiff-Qightofthe two tjwiiffractedsignals (doublet separation as deGned in the satellite-pulse observation technique) and the reflector depth (or length).

The result was an accurate estimate of the through-wall dimension (or length) of the reQector depending on which

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diffracted signal pair was being producecL The amplitudeWop technique was applied to the C-scan data using the time~f-Qight technology to estimate Qaw length.

While it was recognized that readily detectable ti~iffracted waves are not necessarily gener-a

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ated horn real Qaws in every case to provide time~f-Qight Qaw-sizing information, it was ant+-

pated that using a combination of the focused transducer and timewf-Qight techniques would provide accurate sizing of the planar Qaws in question.

C. Test Mockups In order to adequately test and qualify these two special approaches, it was necessaty to build realistic mockups ofthe nozzle geometries in question. Itwas determined that two mockups would be fabricated, one representing the inlet/outlet nozzle configuration and the other, the core-Qood,

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or safety-injection, nozzle.

These mockups were fabricated from forged material suniiar to that used in the actual nozzles of the RPV. A 9Megree section mockup of the inlet/outlet nozzle (Figure 4) and a full360-degree core-flood nozzle mockup (Figure S) were built. Six planar Qaws were placed in the inlet/outlet mockup, and Gve planar Qaws, in the core-flood mockup (see Table I),

The Qaws consisted of machined notches and Qat-bottom holes placed at locations representing the nozzle-to-shell weld fusion line nearest the nozzle bore.

The planar Qaws were chosen because these most accurately represented the Qaws detected in the nozzle-to-shell welds in question and other excavated and conGrmed nozzle fabrication Qaws.

(See Appendix A for a disamion about the nozzle-to-shell weld flaws.)

Haw sizes ranged from '1 percent t '(through-wall thickness) (0.094 inch) in the through-waII dimension of the RPV weld by approximately I/2 inch in length, to 12 percent t (1.093 inches in diameter) in the through-wall dimension (Qat4ottom hole).

1'n each mockup, two small notches

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Table 1

SIZE OF REFLECTOR MACHINEDINTO THE CORE-FLOOD ANDINLET/OVTj~MOCKUPS (measured to the nearest thousandth of an inch)

Core-Flood Mockup ReQectors:

t Inlet/Outlet Mockup ReQectors:

0.188 x 1.00 0.188 x 0500 (two reQectors) 0562 x 1.093 1,093 dia. round Qat-bottom hole 0.094 x 0500 0.188 x 0500 0.188 x 0500 (two reQectors) 0562 x 1.093 1.093 dia. Qat-bottom hole (twin Qaws) were placed in close proximity to determine the ability of the applied transducer-technique combinations to separate the individual Qaws.

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D. Technique Evaluation Once the techniques were chosen and the transducers and mockups built, a comprehensive scanning program was performed using Geld examination and positioning equipment as well as Geld recording equipment to perform the Qaw-sizing exercises.

The mockups were placed in the SwRI scanning tank (used for the uncontaminated PaR Device), and several sets of scans were made on each mockup Qaw. The scan data were recorded and analyzed on the Sw RI EDAS color-imaging ultrasonic system, and the size estimates for each Qaw were compared to the actual sizes of the Qaws in the mockups.

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Several different focused-beam transducers were used on both the inlet/outlet and the core-Good nozzle mockups to determine the best transducers.

Based upon these studies, focused trans-ducers were chosen for each type of nozzle. The optimum inlet/outlet nozzle transducer was a 3-

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by 3-inch piezoelectric crystal that focused in both the axial and circumferential directions.

The optimum core-Qood nozzle transducer, which also focused in both the axial and circumferential directions, contained a 1-by 3-inch piezoelectric crystaL 'Ihe frequency of both transducers was 5 MHz.

Identical search-unit module designs (a 35-degree longitudinal-wave search unit for axial scanning and Qaw-depth estimation and a 454egree longitudinal-wave search unit for circumfer-ential scanrung and Qaw-length estimation) were adopted for both nozzles by the timewf-Qight technology, The frequency of both transducers was 5 MHz.

In order to compare the special sizing procedures with the beam-spread sizing procedure

{ASMEtechnology) used in the past, it was necessary to perform scanning with standard detection transducers and size the Qaws,

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1 The actual Qaw sizes and the size estimates obtained using the three different Qaw-sizing technol-ogies are shown in Tables 2 and 3.

Table 2 DEPTH X LENGTH ESTIMATES {IN.)OBTAINED BY THE ASME CODE, FOCUSED-BEAM, ANDTIME-OF-FLIGHTPROCEDURES FOR THE FIVE CORE-FLOOD, OR SAFETY-INJECTION, NOZZLE FLAWS Actual Raw Aiz!UJJE3 0.19 x 050 0.19 x 050 0.19 x 1.00 056 x 109 1.09 round e

OA4 x 1.15 036 x 1.15 0.69 x 230 1.05 x 255 1.05 x 255 S'

ti ates sed i

028 x 0.79 028 x 0.79 092 x 1.07 0.60 x 121 1.08 x 136 eo t

020 x 0.75 020 x 035 025 x 120 055 x 0.95 1.10 x 120, 10

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Table 3 DE~ X LENGTH ESTTMATES gN.) OBTAINEDBY THE ASME CODE, FOCUSED-BEAM, ANDTIME-OF-FLIGHTPROCEDURES FOR THE SIX INLEI'/OU1l~NOZZLE FLAWS Actual Haw AzHirQ 0,09 x 050 0.19 x 050 0.19 x 050 0.19 x 1.00 056 x 1.09 1.09 round 038 x 121 1.66 x 2.11 1.18 x 222 2.05 x 2.44 256 x L55 S

036 x 055 032 x 0.48 0.40 x 0.48 050 x 120 0.64 x 1.10 1.60 x 124 0.10 x 0.65 020 x 0.45 0.20 x 055 020 x 0.95 0.60 x 120 1.15 x 120 E.

Procedure Development Once the Qaw-sizing data were analyzed, the transducers and the techniques were incorporated into special Geld procedures to be used for Qaw sizing during the upcoming R. E. Ginna RPV examination.

F.

Evaluation of the Framatome Focused Search Vnits Two Framatome focused search units were delivered to SwRI for possible evaluation on the inlet/outlet and core-Qood nozzles.

One unit with a 2-MHz transducer was not evaluated due to an inherent design problem and time constraints on the PaR Device.

The search unit was con-structed with a plastic sheath holding the various elements together. Itwas determined that the

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plastic sheath must be replaced by a metal one to erLsure struwua1 integrity. The second Frama-tome search unit, with a 4-inch diameter and 2.4-MHz frequency traducer, was tested on the inlet/outlet nozzle.

The transducer was operated at the design conditions of a 4-inch standoff distance at 15 degrees.

The results of the EDAS data analysis showed greatly oversized defects.

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For example, the data on the 0562 by 1.093-inch notch showed that at 10 percent (or 20 dB down),

the estimated size was 0.88 by 652 inches; at 25 percent (or 12 dB down), estimated size was 0.68 by 4.96 inches; at 50 percent (or 6 dB down), estimated size was OA4 by 239 inches. Data on the other notches illustrated similar oversizing. The problem appeared to be related to the frequency ofthe transducer, since the 225-MHz focused data acquired during this project compared with the 5-MHz focused data showed similar overestimation of the defect size.

IV. RESULTS As evidenced by the data in Tables 2 and 3, Qaw sizing using both special procedures produced extremely good results.

The amplitude<rop point chosen for focused+earn sizing was 25 percent of maximum signal amplitude; it was chosen speciaHy for the purpose ofyielding slightly conserva-tive results.

The data showed that with this 12MB drop sizing criterion, none of the Qaws in the two mockups were undersized.

For the core-Qood mockup Qaws, the maximum oversizing in through-wall dimension was 0.13 inch.

For the inlet/outlet nozzle mockup Qaws, the maximum oversizing in through-wall dimension was 05 inch. The mean errors of overestimation for the core-Qood and inlet/outlet nozzle mockup Qaws were 0.1 inch and 02 inch, respectively.

Length measurements were within 03 inch of actual length.

The satellite-pulse observation technique ofthe timewf-Qight technology was applied to the B-scan data obtained for the eleven mockup Qaws with the axially scanned transducers to estimate Qaw depth.

Maximum oversizing in the through-wall dimension was 0.1 inch.

The amplitudeWop technique of the time-Qight technology was applied to the Cancan data obtained for the eleven N i mockup flaws to estimate their length. 'Ihe length estinuttes were within 02$ inch of their actual values (%hpercent conQdence level).

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V. CONCLUSIONS The project was very successful In every case, the focused-beam and tim~f-Qight techmques yielded much more accurate sizing results than those obtained using the Code tectuuques.

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anticipated that with the completion of the project and qualification of the new technologres, the disposition of Qaw indications of this nature vali be much more straightforward and acceptable to the regulatory bodies in future exanunations.

The proceduralization of the employed transducer-technique combinations and available imaging equipment willalso assure that the sizrng of planar Qaws willbe more clearly deGned in the documentation.

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ATTACHMENT 5 STRUCTURAL INTEGRITY LETTER

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S, INC.

aden Expressway Suite 226 San Jose, CA 95118 (408) 978-8200 TELEX: 164617 S1RUCT FAX: (4081 9784964 April 26, 1989 ZFC-89-034 SIR-89-026, Rev.

0 Fossil Plant Operations 66 South MillerRoad Suite 10 Akron, Ohio 44313 (216) 864.8886 FAX:(216) 669.5461 Michael J. Saporito Rochester Gas

& Electric Corp.

R. E. Ginna Nuclear Power Station 1503 Lake Road

Ontario, NY 14519

Subject:

ASME Code Section XI Acceptability of the "B" Inlet Nozzle Flaw Indication in the R.E.

Ginna Reactor

Vessel, Based on Spring 1989 Inservice Inspection Results

Dear Mike:

The subject inservice inspection (ISI) flaw indication has been evaluated by us as acceptable in accordance with ASME Section XI for continued service without repair, as shown on the attached calculation package sheets.

Since the flaw, interpreted as an original construction slag defect at approximately midwal1 of the nozzle-to-vessel weld, is shown by the present UT examination to be smaller than when it was evaluated as acceptable by.Teledyne in 1979, that earlier report conservatively bounds the current flaw evaluation.

In summary, our attached flaw evaluation supports the following conclusions:

Irradiation effects from the core are negligible at the flaw location, 2.

The applied fracture mechanics K for the embedded flaw with a

through-wall dimension of 0.48 inches and a

length of 4.94 inches is calculated as 7351 psi.~a.n.

due to the pressure loading and weld residual stresses described in the Teledyne report, 3.

The above K provides a margin of 27.2 against an upper shelf reference K (KIR) of 200, 000 psi. ~an.,

compared to a Section XI recpxired margin of 3.16, and 4

Predicted fatigue crack growth, verified by the ISI experience, is negligible.

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M. Saporito April 26, 1989 JFC-89-034/SIR-89-026 Please let me know if you require further information.

Very truly yours,

/6~2 Grfel~/

J.F.

Copeland Associate Reviewed by:

S.

S.

Tang

/mc attachment cc: John F. Smith

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ATTACHMENT 6 STRUCTURAL INTEGRITY ANALYSIS

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25'nd the radius from the nozzle centerline to the defect location is 25" (Teledyne report),

at least an additional 25" can be added to the above 25" number to place the defect at least 50" above the top of the core. lt was verified [3]

that the defect is, in fact, 57" above the core assembly.

From Figure 2-3 (attached)

[8], it can be seen that this gives a multiplying factor of less than 10 times the peak fluence.

From the latest Ginna surveillance report (WCAP-10086)

[8], the peak measured fluence at the vessel inner surface is 4.03 x 10 n/cm for 32 EFPYs.

Thus, the End-of-Life fluence at the defect location is conservatively established as:

(4.03 x 10 n/cm

) x 10 4

03 x 1016 That value of fluence is below the threshold for consideration of degradation of toughness by irradiation

damage, in accordance with

10CFR50, App.

H.

(No surveillance, etc.

is required for locations with EOL fluence less than 10 n/cm Note that the ISI defect is 17 2

at about mid-wall, and would see even less fluence.

Thus, the upper shelf K>R value of 200 ksi ~zn.

used in the 1979 Teledyne report and in WCAP-8503 is still appropriate, since the beltline P-T limits assure that the inlet nozzle will be on the upper

shelf, as stated in the Teledyne report.

Prepared by.

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KIR 200,000 psi ~an for the inlet nozzle ATIGUE CRACK GROWTH The fatigue crack growth law for subsurface

cracks, from ASME Section XI, is:

= 0.0267 x 10 hK dN where da/dN is in./cycles and h,K is in ksi ~z.n.

From prior calculations in this

package, the SKI due to going from 0 to 2500 psig is:

KI kK 0 ~ 86 (6I 868)

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= 5907 psi ~an.

Substituting this hK into an equation to account for mean stress due to the residual stress gives:

effective where:

m =

R = 0.5 K

~ /K mz.n max 1444/7351 0.2

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K ffect tv

= 5907/(1-0.2)

= 6604 psi ~an.

= 6.604 ksi ~z.n.

Substituting Keffective into the da/dN law to gain an estimate of crack growth rate gives:

Prepared by.

Checked by.

File No.

Page ol /3

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da/dN = 2.67 x 10 (Keffe t

)

= 3.03 x 10 in/cycle Even assuming 1200 full pressure cycles (0 to 2500 psig) in the 40 year life of the plant (30/yr.),

which is conservative, as shown on the attached tables of transients

[7,9],

the predicted crack growth for 1200 cycles is insignificant:

ha = (1200) (3. 03 x 10

)

3.6 x 10 in.

The above value is not enough to change the value of bK and the crack growth rate is relatively constant and insignificant.

As mentioned in the Teledyne report [6], thermal stresses at this mid-wall location are expected to be insignificant.

CODE SAFETY FACTORS The Code (Sct. XI) requires a safety factor of The'ctual safety factor in this case is KIR 200 000 KI 7,351

27.2 CONCLUSION

The subject ISI indication is acceptable in accordance with ASME Section XI.

No repair is necessary.

Since the indication is currently shown as smaller in 1989 than it was in 1979, the 1979 analysis and report submitted to the NRC conservatively envelopes the evaluation of this indication.

Prepared by.

Checked by R1e No.

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REFERENCES:

1.

ASME Code, Section XZ, 1983 edition or 1986 edition.

2. Telecopy, M.

Saporito (RG&E) to J.

F.

Copeland (SI),

4-6-89.

3. Letter J.

F. Smith (RG&E) to J.

F. Copeland (SI), 4-11-89.

4. Letter, J.

F. Smith (RG&E) to J.

F. Copeland (SZ), 4-12-89 5.

CAD Drawing of Ginna Inlet N2B Nozzle Weld Showing ISI Indication Location, J.

F.

Smith (RG&E) to J.

F.

Copeland (SI ), 4-23-89

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6.

"ASME Section XI Fracture Mechanics Evaluation of Inlet Nozzle Znservice Inspection Indication," Teledyne Technical Report No. TR-3454-1, R.E.

Ginna Unit No.

1 Reactor Vessel, March 15, 1979.

7.

W.

K.

Ma, "ASME ZIl, Appendix G Analysis of the Rochester Gas

& Electric Corporation, R.

E.

Ginna Unit No.

1 Reactor Vessel",

Westinghouse WCAP-8503, July, 1975.

8. S.

E.

Yanichko, et al, "Analysis of Capsule T

from, the Rochester Gas and Electric Corporation R.

E.

Ginna Nuclear Plant Reactor Vessel Radiation Surveillance Program",

Westinghouse WCAP-10086, April 1982.

9. "Thermal Transients and Categories,"

Ginna Nuclear Power

Plant, Appendix H, RG&E, July 15, 1975.

Prepared'.

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t=9.25" t/2=4. 625" Col7lblned

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APPENDIX A NONMANDATORY Hg h.3300-1 0.5

<em+ ob) I oys 0.4 1.0 Ck 03 0

alt:>>

0.8 03 0

0.1 0,Olla 0

0.6 08 1.0 12 1.4 1.6 Flaw Shape Parameter 0 2.0

{a) Surface Flaw 2a (b) Subsurface Flaw oys specified minimum yield strength major axis of ellipse circumscribing the flaw FIG. A-3300-1 SKAPE FACTORS FOR FLAW MODEL Prepar,"d b" t'T.

~r Clmkcd hy Rhea.

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SECTION XIDIVISION I 1983 Edition f

'l 1.6 Point 1 2e Point 1

~ 0.65 2et 1.4 o

8 13 w

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E 12 Point 2 Point 1 Point 2 Point 1 Point 2 Point 1

0 0.55 2a a 0.45 t

2 ~035 t

Point 1

~ 025 t

~/roy 1.0 0

02 Point 1 03 Point 2 Point 2 0.4 0.6 Flaw Eccentricity Ratio 2e/t t

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wall thickness e

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eccentricity Point 1

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outer extreme of the minor diameter of ellipse (closer to surface)

Point 2

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inner extreme of the minor diameter of ellipse (further from surface)

E FIG. A-33¹2 MEMBRANE STRESS CORRECTION FACTOR FOR SUBSURFACE FLAWS 270 PTgl)jfgd bV'(7~~~

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l0 l5 20 25 30 DISTANCE FROM FUEL CORE ASSEMBLIES (INCHES)

Figure 2-3.

Distance Versus Multiplying Factor for Peak Fluence /pe 2-5 Pfc98t'gf bus Cheered S

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COLD. hEG TEMP RANGE FOR TRANSIENTS CLOSURE HD, BELTLINE, LOWER HD LOW ~')

HIGH

('F)

O')

TABLE 24 TRANSIENTS VS TEMPERATURES $7/

HOT LEG TEMP

,RANGE FOR OUTLET NOZZLE LOW ~1)

HIGH t'F)

O')

Heatup

~2)

- Cooldown Plant Loading &

Unloading Small Step Load Decrease Small Step Load Increase Large Step Load Decrease Loss of I.oad Loss of Power Loss of Flow Reactor Trip From Fuil Power Turbine Roll Steady State Fluctuations Cold Hydro (2)

Hot Hydro 70 527 529 497 475 70 547 550 70 70 599 599 5B3 492 475 70 50 607 612 615 612 633 627 613 607 610 70 corn rison; hi~er limits are for reference only.

NOTE {1) s Use the lower temperature for KI~ curve comparIson, NOTE (2):

These transients are structured to ensure compliance wi p.

lance with Appendix G.

PrGp8)c+ by Chec~xgf p~

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Operating C cle TABLE 2-9 TRANSIENTS CONSIDERED IN SUBCRITICAL CRACK AND ACCUMULATOR I INES (REFERENCE Occurrences in 40

r. Desi n Life GROWTH RATE ANALYSES FOR PRESSURIZER SURGE 7 1.

Startup and Shutdown 2.

Large Step Decrease in Load (with steam dump) 3.

Loss of Load (without immediate turbine or reactor trip) 4.

Ioss of Power (blockout with natural circulation in Reactor Coolant System)

S.

Loss of Flow (partial loss of flow, one pump only) 6.

Reactor Trip from Full Power 7.

Hydrostatic Test (before initial startup, and post operation) 8.

High Head Safety Injection 200 200 80 40 80 400 50 1105 Assume 1200 Significant Cycles in 40 yr.

Design Life (30 cycles/yr.)

Pf(Jpp<Q $y ir r

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RGE-02-004 Revision 0

39

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