ML20203P683

Responds to NRC Questions Re Welds on Lid of Liner.Design of Part 47 Changed to Provide Retention of Valve During Hypothetical 30 Ft Drop.Encl Rev to Stress Analysis Demonstrates Functional Adequacy.W/Three Oversize Drawings

ML20203P683
Person / Time
Site:	07105942
Issue date:	04/10/1986
From:	Schwoerer F NEUTRON PRODUCTS, INC.
To:	Macdonald C NRC OFFICE OF NUCLEAR MATERIAL SAFETY & SAFEGUARDS (NMSS)
Shared Package
ML20203P684	List: ML20203P683 ML20266D720 ML20266D725 ML20266D730
References
26779, NUDOCS 8605080025
Download: ML20203P683 (27)

Text

,

RETURN TU '3%6 YS neutron PRODUCTS inc 22301 Art. Ephraim Road, P.O. Box 68 Dickerson, Ataryland20842 USA 301/349-5001 TWX: 710-828-0542 April 10, 1986 Mr. Charles E. MacDonald, Chief g

Transportation Branch h

bEa 01986 > $

Office of Nuclear Material Safety and Safeguards 2

U.S. Nuclear Regulatory Commiesion

• s.WCgggtcpW

~

Uashington, D.C. 20555 ccS*S$0"

/0 oss Ref: (1) Certif icat e of Compliance t'o.,,59.42 -

4 (2) Neutron Productc~ submit'tal dated April-1, 1985-

'~

Dear Mr. MacDonald:

This letter is in response to questions. casked by your staff relative to welds on the lid of the liner.

The design of part #47 on the enclosed NPI drawing-240139 has been changed to provide retention of the valve during a hypothetical 30 foot drop, even it no credit is taken for the weld that attaches part #27 to the lid. The functional adequacy is demonstrated in the enclosed revision to the stress analysis.

The adequacy of the circumferential welds that attach parts #54 to the lid has been demonstrated for each liner constructed by pressurizing the liner to an internal pressure of 175 psia. This imposed a structural loading on the weld greater than what would result-f rom '4' hypothetical 30 f oot drop, as demonstrated in the enclosed stress analysis. In addition, the welds were inspected for leakage at that internal pressure and,found to have no leakage.

q Other welds, made without filler metal, do no,t. affect the leak tightness of the liner and are therefore acceptabl's.' il' eld symbols on NPI drawing 240139 have been clarifled.

- -~

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-- Very'trufy^yours, NEUTRON PRODUCTS, INC.

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APR i 0 t986

• Frank Schwoerer, Vice President

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.I ENCLOSURE 3A, Rev.2 ANALYSIS OF LINER INTEGRITY This enclosure discusses the integrity of the liner (including the bolted closure and the valves and fittings on the top plate), for normal conditions of

- transport and hypothetical accident conditions..This enclosure supplements the analyses described in Enclosure 3.

~

A. Normal Conditions -' Bolted Closure The analyses described in this section follow the methodology of Appendix II~

(Rules for Bolted Flange Connections)'to Section VIII, Division 1 of the ASME Boiler and Pressure Vessel Code. The calculations are done in accordance with-the procedures for flanges with ring type gaskets, because that is the type of gasket used. The. shim in the liner closure is designed to~ carry essentially no load during bolt up and normal operating conditions. These analyses are applicable to initial boltup and conditions seen by the liner under normal conditions of transport. Potential free drops under normal conditions of I

transport are enveloped by the free drops analyzed as hypothetical accident conditions in the next section. The development-of these results is detailed in D.

4

1. Material Properties

~ 1 Liner and flange material (304 SS plate, ref: Subsection C of ASME VIII) i (1000F

<5000F Tensile strength 75,000 psi Yield strength _

30,000 Vorking allowable strength 18,800 (S )

12,100 (S )

a d

Bolt material (Unbrako 1960 Series alloy steel, or equivalent)

Tensile strength 180,000 psi Yield strength 155,000 Working allowable strength 50,000 (S )

>40,000 (S )

a b

In order to limit the torque that must be applied by a long-handled-tool, 4

the bolt-up stresse will be limited to:

l Bolt-up stress 30,000 (S ')

a

2. Bolt Loads (ref: UA--49, ASME Section VIII) i i

It is necessary to examine two separate and independent conditions, as follows:

Operating conditions:

o l

Vml = 0.785 G P + (2b x 3.14 G m P) = 24,791 lbs.

2 i

where: P = design pressure = 150 psi I

b = effective seating width of gasket =.293 in.

l G = dia at gasket load resction = 11.414 in'.

l m = casket factor = 3.0

ENCLOSURE 3A, Rev.2 Analysis of Liner _ Integrity _.

Page No. 2 Gasket seating:

Um2 = 3.14 b G y = 105,011 lbs

.where: y_=. gasket seating _ load = 10,000 psi (ref: Table UA-49.1)

3. Required Bolt Area (ref: UA-49)

The required total bolt area is the larger of the following:

Am1 " Uml/Sb Am2 = Vm2/S '

a where S ' is'the bolt-up stress, used instead of S as specified by a

a ASME Section VIII, and S and Sb are the allowable working stresses.

a Thus:

2 Am1 = 24,791/12,100 = 2.05 in 2

Am2 = 105,011/30,000 = 3.50 in The latter case (gasket seating) governs.

2 The bolt area at the base of the threads is.785 (.620)2 =. 302 in,

2 The total bolt area (A ) = 12 x.302 = 3.62 b

in, which exceeds'the I~,

required bolt area.

4. Flange Design Bolt Load (ref: UA-49) c Operating conditions:

=Vml = 24,791 lbs Gasket seating:

= 1/2,(Am2 + A ) Sa = 106,800 lbs b

5. Flange Moments (ref: UA-50)

Operating conditions:

l M=MD+MT+MG = 29,060 in.lb Gasket seating:

M = 104,717 in Ib

~

6. Flange Stresses (ref: UA-51)

Operating conditions:

Stress Allowable Sfty Fctr*

Longitudinal hub stress = 5,202 psi 18,100 psi 3.5 Radial flange stress =

131 12,100 92.

Tangential flange stress = 3,662 12,100 3.3 (S +S )/2 =

2,667 12,100 4.5 H R (S +S )/2 =

4,432 12,100 2.7 H T

• Acceptable value = 1.0 or greater i

e

.x.......

.. ENCLOSURE 3A, Rev.2__ _. _

Analysis of Liner Integrity Page No. 3 Gasket seating:

Stress Allowable Sfty Fctr*

Longitudinal hub stress = 18,744 28,200 1.5 Radial flange stress =

471 18,800 40.

Tangential flange stress = 13,194 18,800 1.4 (S +S )/2 =

~'

9,608 18,800 2.0 H R (S +S )/2 =

15,969 18,800 1.2 H T

• Acceptable value is 1.0 or greater

7. Stresses in Top Plate The boltup loads impose a bending moment on the top plate and, as a result, a maximum bending stress of 6,383 psi. The allowable working stress of the material is 18,800 pai and the Safety Factor to the allowable working stress is 2.9.

8. Bolt Torque The required bolt torque is established by the gasket seating condition.'A tentative value, based on data provided by Unbrako, is 1320 in.lb. The actual value will be established in the course of pressure testing the first liner, prior to the first shipment, by measuring the torque required to compress the gasket to its nominal seated thickness of 0.100 in. or whatever is required to prevent leakage of helium at the design pressure of 150 psig. That experimentally determined torque will be used when sealing the liner for shipments.

9. Vibration The GE 700 cask and the liner are shipped in an upright position. The only type of vibration that potentially threatens the integrity of the liner and bolted closure is a lateral, rocking motion in which the edge of the top plate impacts the inside of the cask cavity. This would imp,ose a shear loading between the top plate and flange of the liner, which would be resisted by friction between the heads of the bolts and top plate and by shear and bending loads in the bolts. Any vibration that may occur will be damped by friction between the liner and sleeve and by relative motions of the contents of the liner. It is estimated that the maximum lateral vibrational impact loading will be no greater than.lg, which is a factor of approximately 50 below the loading that could cause relative motion between the top plate and flange. Therefore, the integrity of the liner is not threatened by vibration incident to normal conditions of transport.

B. Liner Integrity - Ilypothetical Accident Conditions

1. Free Drop Upside-Down Impact j

In an upside-down' impact, the contents of the liner (180 lbs) transfer thair load directly to the central portion of the top plate. The load is

• essentially uniformly distributed. The top plate itself and its

m~.

ENCLOSURE 3A, Rev.2 Analysis of Liner Integrity Page No. 4 appurtenances weigh 115 lbs. The loads from the bottom'of the liner (135 lbs) and the sleeve (240 lbs) are transmitted to the top plate through the shim ring. The maximum compressive stress in the shim ring for a 278g impact is 3,363 psi. The maxim,um compressive stress in the liner wall is

~3950 psi. The yield stress at 400oF is 20,700 psi and the Safety Factors to yield are 6.2 and 5.2, respectively.

These impact loads impose a bending moment on the top plate opposite in direction from the boltup loads. The maximum combined bending stress in the top plate is approximately 14,000 psi, which is below the yield stress of 20,700 psi. The Safety Factor to yield is 1.5. The deflections at the bolt circle and at the gasket are approximately.001 in, which means that the bolt loading and gasket compression are essentially unaffected.

The isolation valves on the top of the liner are supported by a redundant structure. The load frcm a top-down impact of 278g is carried mainly by a valve support channel. The maximum stress in the channel is a bending stress of 3,805 psi, which gives a Safety Factor to yield of.5.4. The stresses in other portions of the valve support structure are even lower.

The loading on the tube elbow from a top-down impact would be less than the loading that has been imposed by a pressure integrity test. It is concluded, that the valves and fittings will remain in place.

3 The valves and fittings are surrounded and protected from impact by the pa short section of 10 IPS piping and two cross plates, which extend above the tops of the valves. The total cross-sectional area of the pipe and cross 2

plates is 12.8 in. T'he compressive stress in these parts from a 278g top-down impact is 14.563 psi. As the yield stress at 4000F is 20,700 psi, the Safety Factor to yield is 1.4. No inelastic deformation of these structural members will occur and the valves and fittings will not be contact the interior o.f the cask cavity.

In summary, the liner, including the bolted closure and pre,ssure boundary fittings on the top plate, will retain its integrity in cas.e of a 30 ft, free drop with a top-down impact.

Bottom-Down Imoact In a bottom-down impact, the mass of the top plate.is supported by shim ring and the wall of the bottom section of the liner. The contents, bottom plate of the liner, and sleeve do not impose loads on the closure or liner wall. The maximum compressive stress in the shim for a 278g impact is only about 1000 psi. The maximum compressive stress in the liner wall is.10,179 psi. Both af these values are within the yield stress at 4000F (20,700 psi) and the Safety Factors to yield are 20 and 2.0, respectively. The moment on the top plate is opposite in direction and smaller than the moment from the boltup loads. The resultant stresses and the deflections at the bolt circle and gasket are npgligibly small. The bolt loading and gasket compression are essentially unaffected.

A bottom-down drop subjects the valves and fittings on the top plate to

' lower loadings than described above for a top-side down impact and will not l

violate the pressure boundary.

I ENCLOSURE 3A, Rsv.2

-Analysis of Liner-Integrity--

Page No. 5 In summary,'the liner, including the bolted closure and fittings on the top plate, will retain its integrity in a 30 ft. free drop with a bottom-down impact.

Side-Down Impact In a side-down impact, the assembly clearances are such that the edges of the flange and top plate could impact the wall of the cask cavity before the body of the liner obtains lateral support from the sleeve. In this case, there is a potential shear loading in the liner wall just below the flange, from the mass of the liner and its contents. The resultant stress from a 270g impact is 13,770 lbs, which is less than the ultimate shear strength of the material at 4000F (35,400 psi). The corresponding Safety Factor is 2.6.

A side-down impact would impose a shear loading and moment on the supports of the valves on the top plate. The loads are resisted mainly by the the hold-down channel over the valve body. The maximum shear stress is 7,613 psi. As the yield stress in shear at 4000F is 11,385 psi, the Safety Factor to yield is 1.5. The load transmitted to the results in a maximum bending stress of 6,012 psi, which corresponds to a Safety Factor to yield of 3.4, and a shear loading in the channel attachment welds of 3,507 psi, which corresponds to a Safety Factor to yield of 3.2. This demonstrates that the valve will remain in place.

In summary, the liner will retain its integrity in a 30 ft. free drop with side-down impact.

Oblique Impacts An oblique, e.g.,

corner, impact of the shipping packare will result in larger distortions and hence lower g loads than postulated for the other impacts discussed above. The loadings on the liner and itsl appurtenances can be regarded as superpositions of fractions of the loadi'ngs described above and the total loads will be lower. Therefore, the liner will retain its integrity.

2. Hypothe$tical Fire As described in Enclosure 3, the maximum temperature of the lead in the cack is 4640F, which indicates that the liner, bolted closure and gasket, and valves and fittings on the top plate will have a maximum temperature of no more than 5000F.

All of the materials, except the asbestos filler in the gasket and the head bolts, have the same coefficient of thermal expansion. All parts of the bolted closure will be at essentially the same temperature, because the heat flux through the top of the' liner is negligible and stainless steel has a relatively high thermal conductivity. The differential thermal expansion between th'e neck of a bolt and thickness of the top plate is 3 approximately.0016 in, and is in the direction of increasing the gasket seating force. The bolts have ample margin to assume the additional load.

-ENCLOSURE 3A, Rev.2"

. Analysis of Liner Integrity Page No.-6 The maximum internal pressure in the liner will be 30 psig (ref: Enclosure-3), which is well bplow the design pressure of 150 psi and the rated pressure of the ga.sket (250 psi). Based on data from the gasket

~

the '_ gasket will, retain its function up to 10000F.

manufacturer, All of the parth of the valves and fittings on the top plate, that comprise the pressure boundary, are stainless steel and will retain.their. integrity and sealing function to a temperature of at least~5000F.

In summary; the liner will retain its integrity during exposure of the shipping package to a hypothetical fire as prescribed by 10 CFR 71~.

/

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ENCLOSURE 3A, Rev.2-T nalysis of Liner Inteiriti A

- '~

- ~~

' ' - ~

Page No.~7-Table 1 Summary of Minimum Safety Factors l

Stress Condition Safety' Factor To:

Liner Flange Stress Operating Conditions 2.7 Allowable Working Stress Gasket Seating 1.2 Allowable Working Stress Liner Lid Bending Stress Gasket Seating 2.9 Allowable Working Stress 30 ft Upside Down Drop 1.5 Yield Stress at 4000F

{

Protective Pipe and Plates on Lid 30 ft Upside Down Drop 1.4 Yield Stress at 4000F Liner Wall 30 ft Side Down Drop 2.6 Shear.' Strength at 4000F Valve Supports on Lil 30 f t Side Down 11 rop 1.5 Yield Stress at 4000F

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Tnt.c X.-FLR% tut.A7 Fon Far Pwrts Notati:n: If = total applied I:ad (Ib.); sa = unit applied load (Ib. per:q. in.);i = thickness e f plata (in.);s = unit stress ct surface

. of plata.(Ib..pcr sq. in.);y.=xcrtical deflection of plate hom original position (iu.); o - slope of plate measured from horizo'ntal(ca.1); Z 11 = modulus of clasticity;m = reciprocal of r, Poisson's ratio. g denotes any given point on the nierface of piste;r denotes the distance A cf g from the cente ref a circularplate. Other dimens*ons and corresponding symbols are indicated on figurcs. bitive sign for s Indicates

' tension at upper surface and equal compression at lower surface; negative sign indicates reverso condition. Nitive sign for y indicates, upward deflection, negative sign downward deflection. Subscripts r, f, c. and b used with a denote respectively radial direction, tangential direction, direction of dimension a, and direction of dimension b.

All dimensions are in inches. All logarithras are to the base e, g

(log. z== 2.3026 logi. 2).

(See pp. 215,216 and 218 for stresa and deflection coefficicuts.)

g Ferraulas for st,em anit d.f!,et*ee M

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' '" / 2 ) M LISTING OF-BASIC PROGRAM -TO CALCULATE BENDING STRESSES IN LINER LID 100 REM GE700 LINER, STRESSES IN TOP PLATE 110 CLEAR-123 DIM R(7),SR(7),ST(7),Y(7) 130 DEFINT I 140 FOR I=1 TO 7 150 ' READ 'R (I) -

--~

~_

160 DATA 0,2.65,5.3,5.71,6.688 7.038,7.44 3

170 NEXT I 180 M=1!/.27 : T=1.5 : E=3E+07 : A=R(7) 193 SF=-3/(6.28*M*T^2) 200 YF3=-3*(M^2-1)/(6.28*E*M^2*T^3) 210 YF2=YF3/8!

220 LPRINT "R(IN)","SR(PSI)","ST(PSI)","Y(IN)"

230 LPRINT 240 REM BOLTUP LOADS 253 LPRINT " STRESSES AND DEFLECTIONS FROM BOLTUP" 260 REM LOAD COMBINATION 1 270 R0=13.375/2! : W=105800!

280 FOR I=1 TO 7 290 GOSUB 3000 300 NEXT I 310 REM LOAD COMBINATION 2 320 R0=11.414/2! : W=-106800!

-g 333 FOR I=1 TO 7 340 GOSUB 3000

_350 LPRINT R (I), SR (I), ST (I), Y (I) 360 NEXT I

~

370 LPRINT 380 REM ADD PRESSURE LOADS 390 LPRINT." STRESSES AND DEFLECTIONS FROM BOLTUP PLUS PRESSURE" 400 REM LOAD COMBINATION 1 410 R0=13.375/2! : W=2300!

420 FOR I=1 TO 7 430 GOSUB 3000 440 NEXT I ll 450. REM LOAD COMBINATION 2 460 R0=10.62/2! : W=-2300!

470 FOR I=1 TO 7 480 GOSUB 2000 490 LPRINT R (I), SR (I), ST (I), Y (I) 500 NEXT I

~

510 LPRINT 520 REM ADD LOADS FROM TOP DOWN IMPACT 530 LPRINT " STRESSES AND DEFLECTIONS WITH TOP-DOWN IMPACT" 540 REM LOAD COMBINATION 1 SSD R0=10.59/2 : W=114258!+60048!

560 FOR I=1 TO 7 570 GOSUD 3000 q-SO REM LOAD COMBINATION 2 600 R0=14.13/2 : W=-114258!.

S

/ 3 g /t/.

~ ' '

'~ ~

610 FOR I=1 TO 7

,; 620'GOSUB 3000

~

~

630 NEXT I 64D REM LOAD COMBINATION 3 650 R0=10.42/2 : W=-60048!

660 FOR I=1 TO 7 670 GOSUB 2000%

683 LPRINT_ R.(I), SR(I), ST (I)., Y (I) 690 NEXT I 700 END 2000 REM CASE 2, ROARK TABLE X 2010 IF R(I)) RO.THEN 2200 2020 Pi=M+(M+1)* LOG (A/RO)-(M-1)*RO^2/(4*A^2) 2030 P2=-(3*M+1)*R(I)^2/(4*RO^2) 2040 P3=-(M+3)*R(I)^2/(4*RO^2) 2050 SR(I)=SR(I)+W*SF*(Pi+P2) 2060 ST(I)=ST(I)+W*SF*(Pi+P3) 2070 Pi=4*A^2-5* RO^2+R ( I ) ^4 / RO^2- (8*R ( I ) ^2+4* RO^2)

• LOG ( A/ RO) 2080 P2=-2*(M-1)*RO^2*(A^2-R(I)^2)/((M+1)*A^2) 2090 P3=8*M*(A^2-R(I)^2)/(M+1) 2100 Y (I) =Y (I) +W*YF2* (Pi+P2+P3) 2110 GOTO 2400 2200 Pl=(M+1)* LOG (A/R(I))-(M-1)*RO^2/(4*A^2) 2210 P2=(M-1)*RO^2/(4*R(I)^2) 2220 SR(I)=SR(I)+W*SF*(Pi+P2) 2230 ST(I)=ST(I)+W*SF*((M-1)+P1-P2)

\\

2240 Pl=(12*M+4)*(A^2-R(I)^2)/(M+1) 2250 P2=-2*(M-1)*RO^2*(A^2-R(I)^2)/((M+1)*A^2)

-2260 P3=-(8*R(I)^2+4*RO^2)* LOG (A/R(I))

2270 Y (I) =Y (I) +W*YF2* (Pl+P2+P3) 2400 RETURN

/

3000 REM CASE 3, ROARK TABLE X 3010 IF R(I)) RO THEN 3200 3020 P1=(M-1)/2+(M+1)* LOG (A/R0) 3030 P2=-(M-1)*RO^2/(2*A^2) 3040 SR(I)=SR(I)+W*SF*(Pi+P2) 3050 ST(I)=ST(I)+W*SF*(Pl+P2) q 3060 Pl= (3*M+1) * ( A^2-R (I) ^2) / (2* (M+1) )

3070 P2=-(R(I)^2+RO^2)* LOG (A/RO) + (R(I)^2-RO^2) 3080 P3=-(M-1)*RO^2*(A^2-R(I)^2)/(2*(M+1)*A^2) 3090 Y(I)=Y(I)+W*YF3*(Pl+P2+P3)

~~

3100 GOTO 3400 E

3200 Pl=(M+1)* LOG (A/R(I))

3210 P2=(M-1)*RO^2/(2*R(I)^2) i 3220 P3=-(M-1)*RO^2/(2*A^2) 3230'SR(I)=SR(I)+W*SF*(Pl+P2+P3) 3240 ST(I)=ST(I)=W*SF*((M-1)+P1-P2+P3) 3250 Pi= (3*M+1) * ( A^2-R (I) ^2) / (2* (M+1) )-( R ( I) ^2+RO^2)

• LOG ( A/R (I) )

3260 P2=-(M-1)*RO^2*(A^2-R(I)^2)/(2*(M+1)*A^2) 3270 Y(I)=Y(I)+W*YF3*(Pl+P2) 3400 RETURN g-

--~

...c 0

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0 J

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'infcf [ F ~~

d ANALYSIS-Dir GE700 CASK -WITH-NEUTRON PRODUCTS LINER R ( I N)'

SR(PSI)

ST(PSI)

Y(IN)

STRESSES AND DEFLECTIONS FROM BOLTUP 6382.82 5.501994E-03

- 0

~~~~~ 6382.82~~

6382.82 4.774858E-03 2.'65 6f82.'82

5. 3 6382.82 6382.82 2.593454E-03 5.71 6358.99 0

2.126049E-03 6.688

-431.5991 0

9.181204E-04 7.038

-213.5056 0

4.869167E-04 7.44 0

0 0

STRESSES AND DEFLECTIONS FROM BOLTUP PLUS PRESSURE 0

6934.557 6934.557 5.863322E-03 2.65 6835.131 6879.523 5.075533E-03

5. 3 6536.855 6714.422 2.738558E-03 5.71 6454.433 297.7783 2.242967E-03 6.688

-455.0215 320.9848 9.679457E-04 7.038

-225.0923 294.7991 5.133411E-04 7.44 0

265.6846 0

STRESSES AND DEFLECTIONS WITH TOP-DOWN IMPACT 1

0 4123.919 4123.919 4.972629E-04^,

2.65 1328.11 2576.392 8.931384E-05

5. 3

-6981.948 13872.42

-3.923448E-04 5.71-

-3213.401 12977.26

-3.575273E-04

- a 6.688

-2628.494 10942.58

-1.832279E-04 7.038

-142.8217 10253.62

-9.854301E-05 7.44 0

7024.885 0

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OVERSIZE DOCUMENT

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PAGE PULLED SEE APERTURE CARDS NUMBER OF PAGES: _3 ACCESSION NUMBER (5):

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FTS 492-9999 i

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