ML13191A039

Evaluation of the Monticello Shroud Support Plate Uplift Load with Indications in the H8 and H9 Welds

ML13191A039
Person / Time
Site:	Monticello
Issue date:	05/02/2011
From:	Sowah S, Tang S S Structural Integrity Associates
To:	Office of Nuclear Reactor Regulation
References
L-MT-13-040
Download: ML13191A039 (16)

Text

ENCLOSURE 4MONTICELLO NUCLEAR GENERATING PLANTSUPPLEMENTAL INFORMATION REGARDING CYCLE 25 INSERVICE INSPECTION SUMMARY REPORT -CORE SHROUD SUPPORT FLAW EVALUATION EC-1 8095EVALUATION OF THE MONTICELLO SHROUD SUPPORT PLATE UPLIFT LOADWITH INDICATIONS IN THE H8 AND H9 WELDS(NON-PROPRIETARY VERSION)(15 pages follow)

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~ Structural Integrity Associates, Incy File No.: 1100626.301 tr Project No.: 1100626CALCULATION PACKAGE Quality Program:

E Nuclear El Commercial PROJECT NAME:Evaluation of the Monticello Shroud Support Plate Uplift Load with Indications in the H8 and H9 WeldsCONTRACT NO.:00001005 Release 27, Amendment 001CLIENT: PLANT:XCEL Energy Monticello Nuclear Generating PlantCALCULATION TITLE:Evaluation of Shear Capacity of Monticello Shroud Welds H8 and H9Document Affected Project Manager Preparer(s)

&D on afe Revision Description Approval Checker(s)

Revision Pages Signature

& Date Signatures

& DateA 1 -15 Draft for Client Review Marcos. L. Herrera Preparer:

MLH 4/29/11 S. S. Tang/Sandra Sowah 4/29/11Reviewer:

Hal Gustin/Jay Gillis4/29/1101 -15 Initial Issue Preparer:

Marcos. L. Herrera S. S. TangMLH 5/2/11 SST 5/2/11Sandra SowahSS 5/2/11Reviewer:

Hal Gustin 5/2/11Jay Gillis 5/2/11Gn.taInI Vender Proprietary I r nttilPage 1 of 15F0306-01RI Non-Proprietary.

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AW00Ociates bTable of Contents

1.0 INTRODUCTION

.....................................................................................................

42.0 TECHNICAL APPROACH

.....................................................................................

43.0 ASSUMPTIONS

....................................................................................................

54.0 DESIGN INPUTS .....................................................................................................

65.0 CALCULATIONS

...................................................................................................

65.1 Pressure Difference across Shroud Support Plate ........................................

65.1.1 Top of Shroud Support Plate Pressure Calculation

....................................

65.1.2 Shroud Support Plate Pressure Difference Calculation

................................

75.2 Postulated Crack Profile ..............................................................................

75.3 Limit Load for Shear .....................................................................................

85.3.1 App lied Loads ..............................................................................................

85.4 C rack G row th ................................................................................................

95.4.1 Crack growth in circumferential direction

..................................................

95.5 Evaluation C ases ..........................................................................................

96.0 RESULTS OF ANALYSIS

........

............................................................................

1

07.0 CONCLUSION

S AND DISCUSSIONS

.................................................................

108.0 R EFER EN C ES ......................................................................................................

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Cjsirucmuu h#C orY Asockites, IncList of TablesTable 1: Load Sum m ary ....................................................................................................

12Table 2: Design Input for Shroud Support Plate Pressure Difference Calculation

.............

12Table 3: M aterial Properties at 550 0F ...............................................................................

12Table 4: Pressure Differential across the Shroud Support Plate .........................................

13Table 5: Uplift Load on Shroud Support Plate .................................................................

13Table 6: V ertical Seism ic Load .........................................................................................

13Table 7: Total Upward Shear Force ...................................................................................

13Table 8: Limit Load Evaluation Results for Compound Crack Profile ..............................

14Table 9: Limit Load Evaluation Results for Surface Crack Profile ...................................

14List of FiguresFigure 1. Jet Pumps Inspection Illustration

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1.0 INTRODUCTION

During the Spring 2011 outage, inspection of the Monticello shroud support plate weld H8 and weldH9 was performed.

Visual inspection (EVT1) coverage was obtained from jet pump JP20 to JPI andJP10 to JP 11, as identified in Figure 1 [1]. This accounts for approximately 17% of the H8 and H9circumference

[1]. An additional 64 inches of inspection coverage was acquired with visual inspection VT-3 on the top side of the weld [1] in the area between all the jet jumps. The visual inspection revealed cracking in the shroud support legs but no indications were identified in the welds H8 and H9.This evaluation is performed to quantify the structural margin retaining the shroud support plate H8and H9 welds after one cycle of additional operation assuming plastic collapse in shear to be theapplicable failure mode because the most significant loading is the uplift load due to the verticalseismic and the pressure difference across the shroud support plate.2.0 TECHNICAL APPROACHThe technical approach used for this evaluation is based on the BWRVIP-76

[2], limit load approach.

The limit load analysis for shear failure is developed based on the approach for determining the limitload for an axial crack in the shroud as presented in [2] and summarized below. Consistent with theBWRVIP methodology in [2], the failure mode of the Alloy 600 and corresponding weld materials isconsidered to be the net section (plastic)

collapse, because of the very high ductility of these materials at reactor operating temperatures.

Also, the fluence in this region is not high enough to impact thematerial ductility.

The limit load for an axial crack assuming tensile failure of the remaining ligament is expressed inSection E. 1.2 of [2] as:By similar approach, the shear failure limit load for a crack in a circular weld can be expressed as:(SF)S = oj Lt (2)where: S ý shear force due to uplift loadSF = safety factorFile No.: 1100626.301 C ontains Vener Proprietary-inf-r..atin Page 4 of 15Revision:

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AWssOcjS, WOcasf = shear flow stressL = length of uncracked circumference in circular welds (H8/H9)t = thickness of shroud support plate.Using the maximum shear theory or Tresca criteria, the maximum shear stress at yield is half themaximum yield strength.

The shear flow stress can be expressed as:vsf = Gf/2There are no plant specific safety factors for the Monticello shroud [1]. Per Section D.5 in Reference 2, required minimum safety factors of 2.77 for normal/upset (Level A/B) conditions and 1.39 foremergency/faulted (Level C/D) conditions are used in this evaluation.

In limit load evaluation, elastic-perfectly plastic material properties are used.3.0 ASSUMPTIONS The following assumptions are used:a. Loading in weld H8 and weld H9 is assumed to be pure shear due to the most significant loadsbeing the vertical seismic and the pressure difference across the shroud support plate.b. Material properties of Alloy 600 compatible weld metal are assumed to be the same as theAlloy 600 base metal.c. The shear load is assumed to be evenly distribution between the weld H8 and weld H9.d. The shear load is assumed to be evenly distributed in the remaining ligament of each weld.e. For uninspected region, through-wall cracking is assumed.

This is conservative since no creditis taken for the uninspected region.f. For inspected region, surface cracking with depth of 75% of the plate thickness is assumed.This assumption is based on the general evidence provided by the BWR fleet shroud crackingdata. The flaws generally arrest at 2/3 of the wall thickness, so the assumption of a 75% wallflaw is conservative.

g. The SSE accelerations are twice as large as the OBE accelerations.

h. The vertical flexural shear from the moment induced by the horizontal acceleration due to thejet pump weight on the support plate is assumed to be negligible.

It was estimated that thisupward flexural shear is less than 5% of the total uplift shear load.i. The material is considered to behave in an elastic-plastic manner, which is consistent withBWRVIP methodology for reactor internals in low fluence regions.j. Crack growth in the depth direction is not considered since the assumed crack depth is based onflaw depths observed from BWR fleet operating experience.

Subsequent growth is minimaldue to excellent Monticello water chemistry conditions in the lower plenum.k. Seismic and LOCA are conservatively combined in order to provide added margin to theevaluation and further justify the maximum flaw depth based on BWR fleet operating experience.

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AWOSSoca, Wnc4.0 DESIGN INPUTSThe following dimensions are used in the evaluation:

Reactor vessel inside diameter (ID): 17.167 ft [1]Shroud plate thickness:

2.5 inches [3]Shroud ID: 159.75 inches [4]Shroud thickness:

1.75 inches [4]Design AP across shroud support plate for Levels A through D 100 psi [1]Per Reference 1, the vertical earthquake acceleration is 0.06g.The vessel internal component loads and water loads are obtained from Reference 13 and summarized in Table 1.The input used to calculate the pressure differential across the shroud support plate for different operating conditions are obtained from Reference 7 and summarized in Table 2. The maximum AP forLevel A/B is 29.03 psid for the EPU conditions

[7]. For Level C/D, the maximum AP is 47 psid fromthe 113% OLTP. Since it is not clear if the Level C/D reactor internal pressure difference (RIPD)considers the decompression of the annulus region following a postulated recirculation line break(RLB) event (typically the Level C/D RIPD is given as the main steam line break pressure difference),

a bounding methodology is used in this calculation to calculate an uplift load on the shroud supportplate.Per Reference 1, the Code of Construction isSection III, 1965 with Summer 1966 Addenda [19]. Theallowable stress intensity (Sn) is 23.3 ksi [1]. The material yield strength (Sy), ultimate strength (Sj)and allowable stress intensity for Alloy 600 are obtained from Reference 8 at 550 'F for conservatism and summarized in Table 3. As compared to the allowable Sm from Reference 19 stated in Reference 1, the Sm from different Code Editions remains the same.The input used to calculate the pressure differential across the support plate is summarized in Table 4.The shroud support plate material is Alloy 600 [15].The end of evaluation period (EoEP) is 24 months [1].5.0 CALCULATIONS 5.1 Pressure Difference across Shroud Support Plate5.1.1 Top of Shroud Support Plate Pressure Calculation The pressure at the top of the shroud support plate for normal condition,

Psihoud, is a required input fordetermination of the pressure difference across the shroud support plate for the postulated Recirculation Outlet Break case. Considering hydrostatic

pressure, this may be calculated by:File No.: 1100626.301 Page 6 of 15Revision:

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v sh n I h*t g A. aSciate, c.°fhrOud= Po h (3)1728. vfwhere PO = pressure at the water surface, psiah = water height from top of shroud support plate elevation to the water surface, invf = specific volume of the water at the top of the shroud support plate, ft3/lb =0.021 19ft3/lb (based on annulus temperature, interpolated from [11]).Thus, Pshroud = 1025 + (512.5 -99.25)/(1728 x 0.02119)=

1036.3 psia.The pressure in the lower head is higher than the pressure in the annulus because of the pressure addedby the jet pumps. The pressure difference can be estimated from Reference 7 as the maximumdifferential pressure across the shroud support plate for the Level B condition, which is 29.03 psid.5.1.2 Shroud Support Plate Pressure Difference Calculation A conservative lower bound for the pressure above the support plate is the saturation pressure at theannulus temperature.

A low pressure above the support plate is conservative because it maximizes lifting force on the plate due to the pressure differential across the plate. If the pressure below theplate is held constant and the pressure above the support plate is lessened, the upward force on thesupport plate is increased.

In normal operation, the lowest pressure in the reactor pressure vessel is thepressure in the steam dome. The saturation pressure at the annulus temperature is slightly less than thesteam dome pressure because the annulus liquid is slightly subcooled.

From Reference 7, the maximum Level A/B pressure difference across the shroud support plate isgiven as 29.03 psid. This pressure differential is expected to exist at the instant of the postulated RLBevent.A conservative lower bound for the pressure above the support plate, following the RLB event, is thesaturation pressure at the annulus temperature.

Thus the bounding total pressure difference, AP, for theLevel C/D conditions is given as:AP=Pshoud

-Psat = (1036.3 + 29.03) -886.25 = 179.08 psidThis pressure difference acts to lift the support plate upward.The pressure differentials across the shroud support plate are summarized in Table 4.5.2 Postulated Crack ProfileFrom Reference 1, Welds H8 and H9 were inspected with EVT-1 from JP 20 to JP1 and JP10 to JP 11(about 17% of the circumference),

as shown in Figure 1 [4], with an additional 64 inches inspected File No.: 1100626.301 Page 7 of 15Revision:

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VII~S&NOiauN Inftogi AssociatS, Incwith VT-3. The regions not inspected by VT-3 are the portion of the welds close to the jet pumps, asillustrated in Figure 1 [1].Thus, the uninspected regions are considered to be evenly distributed based on the jet pumps pattern,resulting in 10 uninspected regions as illustrated in Figure 1. These regions are conservatively to becracked through-wall.

Length of weld H8 = 21rtRi=2*1rt(159.75/2+1.75)=

2*iT(81.625) 512.865 inLength of weld H9 = 2rTRo=2*Tr(17.167*

12/2)= 2*rT(103.002)

= 647.18 inTo simplify, an average length for welds H8 and H9 is used for evaluation.

Average weld length for welds H8 and H9 = (512.865+647.18)/2

=580.02 inchThe inspection length inspected by VT-3 for each weld is approximately 64/2 = 32 inches.Using the average weld length, the following are obtained for each weld:Total inspected length = 0.17*580.02+32

= 130.60 inchesTotal uninspected length = 580.02 -130.63 inches = 449.42 inchesThis corresponds to 449.42/10=44.94 inches for each uninspected region.5.3 Limit Load for Shear5.3.1 Applied Loads5.3.1.1 Uplift LoadThe uplift load is due to the pressure difference across the shroud support plate. The AP uplift area(UA) is calculated as:UA = 1"(Ro2-Ri2)=Tr(l103.002 2-81.625

2) = 12399.15 in2The uplift loads due to the pressure difference for Level A/B and C/D are calculated and shown inTable 5.5.3.1.2 Vertical Seismic LoadIn Table 1, it is shown that the total weight of the jet pumps is 10 kips.. Also, the maximum waterweight of 1080 kips from Table 1(b) is selected.

Thus the total weight due to internal structure

&periphery fuel, jet pumps and water weight is:Wt = 189 + 10 + 1080 =1279 kipsFile No.: 1100626.301 Page 8 of 15Revision:

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hxtegdl ~Y AociatS, Inc.The vertical seismic acceleration is 0.06g. This is assumed to be for OBE.The total vertical seismic load for OBE and SSE is summarized in Table 6.The total upward shear force is summarized in Table 7.5.4 Crack GrowthCrack growth in the depth direction is not included since the depth used in the evaluation is consistent with the depths based on BWR fleet operating experience.

In addition, due to Monticello's excellent water chemistry in the lower plenumn, subsequent crack growth will not be significant.

5.4.1 Crack growth in circumferential direction Per Reference 2, the crack growth rate is 5x1 0-5 in/hr. This is used for conservatism regardless of plantspecific water chemistry.

For 10 uninspected

regions, with 2 crack fronts for each region since athrough-wall crack is used, the total crack growth Al for 24 months is:AI= 1O*2*5xl0 5*2*365*24

= 17.52 inchesTherefore, the remaining length of un-cracked circumference at the EoEP isL =130.60 -17.52 = 113.08 inches5.5 Evaluation CasesTwo crack profiles are used to evaluate the structural margin retaining the shroud support plate weldH8 and weld H9. Each of these contains significant conservatisms, which compensate for anyuncertainty in the flaw depths. It is important to note that BWR shroud cracking

history, of whichthere is a significant amount, has shown that typically cracks in shroud welds grow to approximately two-thirds of the shroud wall and then appear to become essentially inactive.

This is particularly expected for Monticello's case because of the excellent water chemistry experienced in the vicinity ofthe indications on the lower side of H8 and H9. These two crack profiles are:(a) Multiple Cracks: A through-wall crack is postulated in the uninspected regions and aremaining ligament of 1/3 of the plate thickness in the inspected region is postulated sinceinspection was performed on the top side only. The 1/3 wall remaining ligament is based onfield experience for BWR shroud welds.(b) Full Circumferential Surface Crack: A surface crack at the bottom plate surface extending along the circumferential length of Weld H8 and H9 with a crack depth at 75% of the supportplate thickness is postulated.

This corresponds to a remaining ligament of 0.625 inches in thesupport plate.File No.: 1100626.301 Page 9 of 15Revision:

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Vjj~hVucuhfIW latoil AWOMOctS, Wnc6.0 RESULTS OF ANALYSISThe limiting shear force due to limit load failure criteria can be calculated using Eq. (2). The flowstress is taken as 3Sm per Reference 9 as used in Reference 20.The analysis results are summarized in Tables 8 and 9 for the two crack profiles described in Section5.5. It is shown that the safety factors are 14.96 and 2.77 for Levels A/B and C/D, respectively for themultiple crack case. For the surface crack case, the safety factors are 57.58 and 10.67 for Levels A/Band CD, respectively.

These are higher than the required safety factors of 2.77 and 1.39 per Reference 2.

7.0 CONCLUSION

S AND DISCUSSIONS An analysis was performed to evaluate the capacity of the remaining length in the Welds H8 and H9 toprevent the up lift of the core shroud. It is shown that, for an EoEP of 24 months, the calculated safetyfactors of for Levels A/B and C/D conditions in Weld H8 and H9 are significantly above the requiredsafety factors of 2.77 and 1.39, respectively, for both conservative flaw configurations analyzed.

These results demonstrate that, even with the postulated flaws in welds H8 and H9, the structural integrity of the shroud support plate is assured.

8.0 REFERENCES

1. Xcel Energy Design Information Transmittal (DIT), "Shroud Support Plate Uplift Analysis,"

Tracking Number EC, Date 5/2/2011, DIT No. 3, S1 File 1100626.207.

2. BWR Vessel and Internals Project:

BWR Core Shroud Inspection and Flaw Evaluation Guidelines (BWRVIP-76),

EPRI, Palo Alto, CA, BWRVIP 1999, TR-1 14232.3. Chicago Bridge & Iron Co. Drawing 35 Rev 5, "Plan of Shroud Support 17'2" ID, 63'-2" INSHeads Nuclear Reactor,"

No. NX-9310-28, SI File 1100626.201.

4. General Electric Drawing 886D487, "Reactor Vessel,"

No. NX7831-7-2, SI File 1100626.201.

5. Not used.6. Not used.7. GEH Report, "Task T0304: Reactor Internal Pressure Differences, Fuel Life Margin, CRGT liftForce, Acoustic and Flow Induced Loads," GE-Hitachi-Nuclear Energy Report GE-NE 0000-0060-9039-TR-R1, DRF 0000-0060-9027, Revision 1, Class III, November 2008.8. ASME Boiler and Pressure Vessel Code,Section II, Part D, 1998 Edition with no Addenda.9. ASME Boiler and Pressure Vessel Code,Section XI, 1995 Edition with Addenda through1996.10. Not used.11. NIST Chemistry

WebBook, http://webbook.nist.gov/chemistry/fluid/.

12. Monticello Drawing No. NX7831-197-1 Revision D, "Monticello Nuclear Generating PlantReactor Vessel & Internals,"

SI File No. 1100626.201.

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VjSftnPWb l Itegfy* AWOMSoi ftsIc13. MonticelloDrawing No. NX7831-7-7 (GE Drawing No. 886D482, Revision 10), "ReactorVessel,"

SI File No. 1100626.201.

14. Not used.15. Xcel Energy DIT No. EC 18095, "Shroud Support Plate Uplift Evaluation,"

Rev.1, SI File1100626.206.

16. Not used.17. BWR Vessel and Internals Project:

Evaluation of Crack Growth in BWR Stainless Steel RPVInternals (BWRVIP-14A),

EPRI, Palo Alto, CA, BWRVIP, 2003, TR-105873.

18. Not used19. ASME, Boiler and Pressure Vessel Code,Section III, 1965 Edition with Addenda to andincluding Summer 1966 Addenda.20. SI Calculation, "Evaluation of the Monticello Shroud with Indications at Welds H8 and H9,"SI File 1100560.301, Rev. 0.File No.: 1100626.301 Revision:

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jS"1"c Wl egi AssocAtes, Wc?Table 1: Load Summary(a) Loads Supported by Internal Shroud Support [13]Component Weight (kips)Internal Structure

& Periphery Fuel 189Guide loads (all fuel, drives, control rods, guide tubes) 397for horizontal earthquake loads onlyJet Pumps 10(b) Water Loads [13]Operating Conditions Water Weight (kips)Normal Full Power 353.1Hot, Stand By 381.4Cold Vessel, Full 729.2Refueling (water level 927") 1080Refueling (water level 655") 651Table 2: Design Input for Shroud Support Plate Pressure Difference Calculation Design Variable Value Units Reference Normal water level elevation, above vessel 512.5 in. 12zeroRecirculation Nozzle centerline elevation, 150 in. 12above vessel zeroTop of the shroud support plate elevation, 98.75 in. 13above vessel zero (1)Annulus Temperature 530.2 OF IAnnulus Saturation Pressure 886.25 psia 11Dome Pressure 1025 psia INote : (1) Calculation based on 108.5" -11.75"+2" from Reference 13.Table 3: Material Properties at 550 'FAlloy 600 Base MetalYield Strength (ksi) 30.1Ultimate Strength (ksi) 80Stress Intensity Sm (ksi) 23.3File No.: 1100626.301 Revision:

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T a bdl e 4 :A P rssuo c ra e i forTable 4: Pressure Differential across the Shroud Support PlateLevel Pressure Differential (psid)A/B 29.03 [7]C/D 179.08Table 5: Uplift Load on Shroud Support PlateLevel Area (in2) Pressure Differential (psid) Up Force (Ibs)A/B 12399.15 29.3 363295C/D 12399.15 179.08 2220440Table 6: Vertical Seismic LoadLevel Coefficient Total Wt (kips) Up Force (kips)A/B 0.06 1279 76.74C/D 0.12 1279 153.48Table 7: Total Upward Shear ForcePressure Vertical Seismic TotalLevel Differential Load (kips) (kips)_________

kips Load___(kips)__

(kips)_____

(kips)A/B 363.295 76.74 440.04C/D 2220.44 153.48 2373.92File No.: 1100626.301 Revision:

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VskkID&W h*y AWOCW~SS, W~Table 8: Limit Load Evaluation Results for Compound Crack ProfileLevel A/B Level C/D(1) EoEP uncracked length (in) 113.08 113.08(2) Support plate thickness (in) 2.5 2.5(3) Remaining ligament (in) 0.833 0.833(4) Available shear area (in') (=(1)*(3))

94.20 94.20(5) Total applied shear load (kips) 440.04 2373.92(6) Applied shear in each weld (kips) (=(5)/2) 220.02 1186.96(7) Tensile Flow Stress (ksi) 69.9 69.9(8) Shear Flow Stress (ksi) 34.95 34.95(9) Shear limited load (kips) (=(8)*(4))

3292.29 3292.29(10) Safety Factor (=(9)/(6) 14.96 2.77(11) Required Safety Factor 2.77 1.39Table 9: Limit Load Evaluation Results for Surface Crack ProfileLevel A/B Level C/D(1) EoEP uncracked length (in) 580.02 580.02(2) Support plate thickness (in) 2.5 2.5(3) Remaining ligament (in) 0.625 0.625(4) Available shear area (in2) (=(1)*(3))

362.51 362.51(5) Total applied shear load (kips) 440.04 2373.92(6) Applied shear in each weld (kips) (=(5)/2) 220.02 1186.96(7) Tensile Flow Stress (ksi) 69.9 69.9(8) Shear Flow Stress (ksi) 34.95 34.95(9) Shear limited load (kips) (=(8)*(4))

12669.7 12669.7(10) Safety Factor (=(9)/(6) 57.58 10.67(11) Required Safety Factor 2.77 1.39File No.: 1100626.301 Revision:

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nrW"uWu h*Oy A Css ,I,'~I50~ ~' 'D'~1~i srp~Ii~,,r

• 4I~f!.~: ~Y'1 ""~U tins c~ Ii. IFigure 1. Jet Pumps Inspection Illustration File No.: 1100626.301 Revision:

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