ML20153H359
| ML20153H359 | |
| Person / Time | |
|---|---|
| Site: | 07109177, 07109179 |
| Issue date: | 04/26/1988 |
| From: | Temus C NUCLEAR PACKAGING, INC. |
| To: | Macdonald C NRC OFFICE OF NUCLEAR MATERIAL SAFETY & SAFEGUARDS (NMSS) |
| References | |
| 24270, VVV8708, NUDOCS 8805120273 | |
| Download: ML20153H359 (7) | |
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April 26, 1988 6
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!!r. Charles MacDonald, Chief 4
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Transportation Certification Branch A
U.
S. Nuclear Regulatory Commission b
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Reference:
Docket Numbers 71-9177 and 91-9179
Dear Mr. MacDonald:
In preparing separate SARs for our Type A Family, some dimensional data was not correctly transposed for the referenced docke t numbers.
The affected pages have been revised.
Please replace the following pages of the above applications with new rev is ed pages listed below, the page numbers are identical for both dockets:
2-12, 2-14, 2-13, 2-16, and 2-21.
If you have any questions please contact me or Robert Smith at (206) 874-2235.
Sincerely, NUCLEAR PACKAGING, INC.
+
w Q q @)"I U~b Charles J.
Temus s3r Technical Director N
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MmPac 10/140 Cask Rev. (, T/88 i
TABLE 2.5.2-1 CASK TIEDOWN CABLE FORCES 10/140 Gros s Weight 56,500 lbs.
Out side Diameter 74.77 in.
Out side Height 83.00 in.
d' 65.6 in, h
65.5 in.
Cable Length, L 71.23 in.
0.278 B,,
B7 0.920 l
B, Cable Tension 254,673 lbs.
6 4
L,
(
P 4
i l
s 1
l i
2-12
NaPas 10/140 Cack Rev. $,4/88
.' f]
From the figure above:
%.s t = 2 in, ed = 2.5 in, d = 2.5 in.
The n:
0 P, = 2(60,000)(2 in. )(2.5 - (2.5/2) cos 40 )
g Using the maximum cable tension of 275,000 lbs, f rom Table 2.5.2-1, the yield Margin of Safety is:
M. S. = (370,200/254,673) - 1 = +.4 5 The cable load consists of bo th horizontal and vertical components, intro-l ducing both a bending moment and a shear load into the outer shell through the
~'T lug to shell weld.
[V The weld stresses in the l ug-t o-sh el l weld are c ompo se d of pure shear and
. ten sion/compres sion due to the moment s.
l Pure shear on weld due to vertical component of the lug load, P:
y h
F, = P / A, y
l The vertical component of force is:
(.920)(254,673) = 234,300 lbs.
P
=
y From Sect ion 2.5.1:
i A, = 32.3 in.2 2-14 i
+--
m--w. - -
w w
3-r- - -em-
--w-
--,,-,c-e---<-------*-,,-w-
, m -- e w y
nT----wy--vr-,---
---cp-v--r- - - - --i-v v e
NmPac 10/140 Cack Rev.$,T/88
)
- Then, F, = 234,300/32.3 = 7254 psi The moment force on the weld is the summat ion of the moments due to the horizontal and vertical component s of the force, or:
M=Fe + P eg y y g
There:
F = 234,3 00 lbs.
y e = 2.5 in.
y Fg = (.278) (254,673) = 7 0,300 lbs.
eg = 4.84 in.
Then, a s sum ing a CCW moment is positive:
M = (234,300)(2.5) - (70,800)(4.84) = 243,082 in-lbs.
Aga in, from Section 2.5.1:
3 z = 122.7 in l
Fg = 243,082/122.7 = 1981 psi Combined Stress:
F, =
((7254)2 + (1981)2 0.5
= 7520 psi j
The lug-to-shell weld Margin of Safety is:
M. S. = (F,/F,) - 1 = (21,000/ 752 0) - 1 = + 1.79 L
l l
(
2-15 1
l---
1 NuPas 10/140 Cask Rev. $,q/88 G
The st res se s induced into the outer shell by the tiedown lugs were determined
/
using the f init e element c.naly s i s program ANSYS, Revision 3, Up da t e 67L, available of the Boeing Computer Services (BCS) Na t iona l Ne two rk, MAINSTREAM -
EKS. The capabilit ies are outlined in Appendix 2.10.5 The analy si s was performed on the ge ome t ry of a rel a t ed cask, the NuPac 14/21011.
The lug and gus set s of that cast are ide n t ical to the 10/140 ca sk, but the inner and outer shells of t h e 14 / 210 a r e.375 and.875 inches, respectively.
Therefore, stresses predicted in these structures are considerably higher than actual stresses that would be occur in the cask.
The 0
Finite Element model consisted of a 45 section of the ca sk outer shell, inner sh el l, cask wall top plate, and on-half the lug.
The length of the cask model below the tiedown lug was suf ficient to eliminate any end (boundary condition) ef fect s f rom af fecting the final results.
To react the lug loads, the nodes along the bottom of the inside and out side shells were constrained from dis-placing vertically.
For symme t ry, the nodes along the se c t ional cut s were constrained from displacing c i rc un fe r e nt i ally and rotating about the X (ra-h dial) and Z (vertical) axes.
%J Springs were introduced between the inner and outer shells at locations where the shells displaced radially towards each other (compres sion only) to account for the pr e se nce of the lead.
The corresponding spring stiffness was estimated for a column of lead as k = AE/L.
Since the purpo se of the springs was to prevent fictitious localized bending stresses, pl a ceme nt of the lead spring was conserva tively chosen as one every four inches.
The model, with exception of the spring elements, was defined entirely of quadrilateral shell el eme nt s.
The ge ome t ry plots are illustrated in Figure 2.5.2-2 to 2.5.2-5.
Figures 2.5.2-2 and -3 have omit t ed the side lug plate for cla ri ty.
The quadrilateral shell el eme n t has bo th bending and membrane stress capabilities with six degrees of freedom at each node:
translations in the nodal x,
y, and z directions and ro t a t ion s about the nodal x,
y, and z axis.
Each element, either triangular or quadrilateral in shape, was defined by four nodes t ha t lie in a plane.
Sections of the model were se gre ga ted by assigned element type nuabe rs.
The thickne s s at each node in an element was defined in a real constant table for each element type.
2-16
NaPas 10/140 C2ck Rev. $, 4/88
' [
The element size was decreased in the area of the lug for greater accuracy.
Fur the rmor e, to e nhance th e model definition, the node directly adjacent to each of the lug attachment nodes was l ine arly constrained to move with that node (e.g., Node 2 was linearly constrained to move with Node 1, Node 14 with Node 13, Nodes 99 and 123 to move with Node 111, etc.) to simulate the pre-se nce of the two-inch wide lug plat e s.
A 281,000 lb load was introduced as a 89,000 lb outward radial component combined with a 267,000 lb downward vertical c ompo ne nt at Node 622.
This is conservatively higher than the cable tension force of 254,673 lbs. from Table 2.5.2-1 for the 10/140 ca sk.
The lug hole was omitted to decrease the com-plexity of the model as any local effects of the hole would not directly affect the reaction of the outer sh el l.
Other than the springs between the inner and outer shells, the contribution of th e le ad strength was neglected.
Also, for con se rva t i sm, the cask wall top plate was de fined as be ing one-half inch thick.
O V
The maximum combined stres s occ urred a t El e me n t 232, directly below the lug, on the outside of the outer shell.
The 20,749 p si combined stress was com-prised of L 22,792 p si compres sive longitudinal stress, a 5004 p si compres sive ci rc un fe r ential stress, and a 164 psi shear stress as shown in Table 2.5.2-2.
A complete nodal d is pl a c e me n t, el eme nt stress, and reaction force output was included on microfiche for the originally approved application for the cask Certificate of Compli a nc e, as Ap pe nd ix 2.10.4.
A co py of this output is available for inspection at Nuclear Packaging, Inc.
A description of how to int e rpre t el eme n t stress output is provided in Appendix 2.10.5.
The se cond highest stres s area in the outer shell occurred around the end of the horizon-l tal lug.
The h i gh e s t, El emen t 88, cont ained a combined stress of 18,203 psi.
l The la rge s t outward radial displacement of the outer shell, 0.0417 inches, occ urred at Node 1.
The largest inward radial di s pl a ceme n t on the outer l
shell, 0.0331 inches, occurred at Node 386.
The Margin of Safety of the outer I
sh el. is:
lO M. S. = (3 8,000/ 20,749) - 1 = + 0.83 l
2-21 I