Abstract:
The structural verification of the LHCb VELO Vacuum vessel
is the subject of this document. Purpose of these calculations
is to investigate stress and displacements in the stainless steel
VELO Vacuum vessel. The Vacuum vessel has to comply with the CODAP Code.
Numerical analysis was performed with the IDEAS TM finite element analysis software.
Design of the vessel
The main difficulty with regards to the structural integrity of the vessel are the openings at both sides.
The openings, in which the detector is mounted, encompass almost the full length of the vessel.
These openings result in a reduction of stiffness of the primary cylindrical shape of the vessel.
Several parts are connected to the vessel: Exit Window, end cover, two Detector Hoods and 2 getter pumps.
Within the document only the end cover of the vessel are considered.
The exit foil is the responsibility of the CERN vacuum group.
The aspects of the two detector hoods will be covered in a different document.
In the analysis only the loads of the connecting elements are transferred to the vessel,
the stiffness of these elements is disregarded. Using these assumptions,
the worst case effects of the elements are regarded in the analysis of the vessel.
The end cap cover is regarded in a similar way.
Operational conditions
The load of the vessel is determined by the weight of the vessel, the connecting elements,
and the vacuum force. The vessel is operated at two temperatures.
The operation temperature and pressure are given by the vacuum procedures.
The conditions for the analysis of the vessel are given in the following table:
Material data:
The vessel and the end cover will be made from AISI 316L
TYPE X2CrNiMo17-12-2 (1.4404).
The material has been selected based on the vacuum requirements and the welding ability of the material.
| | | At 20-25 oC | At 150 oC |
Tensile strength | Rm [MPa] | min. | 585 | 525 |
Yield strength | Rp 0.2% [MPa] | min. | 260 | 230 |
Young's modulus | E [GPa] | min. | 200 | 186 |
Density | [g/cm3] | . |
7.85 | . |
Poisons ratio | . | . | 0.30 | . |
Elongation at break | A5 [%] | min. | 35 | . |
Brinell hardness | HB | max. | 180 | . |
FEA:
A finite element analysis has been done to model the expected stresses and to verify
that these stresses are within the limits defined by the CODAP.
The finite element analysis of both the vessel and the end cover where done
with the finite element analysis module of Ideas.
For both parts a stress- and a buckling analysis where made. Presented are a description of the models,
the results and the interpretation of the results.
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Half the vessel is modeled, as the vessel is symmetric about YZ, see the figure
at the right. The boundary conditions for the model are given by the loads on the vessel,
the reaction forces from the support of the vessel, and the symmetry constraints
At the flanges no bending moments are introduced, the connecting elements at the flanges
are given sufficient stiffness to avoid the transfer of a bending moment at the flanges.
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Finite Element Mesh |
Vessel | End Cover |
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Mesh types:
3D Solid parabolic tetrahedron
2D Thin Shell parabolic quadrilateral
Safety Factor:
Following the chosen construction class C and welding coefficient z=0.7, the stress limits according to CODAP are:
- Global zones:
| fg = Rm/3.5 = 525/3.5 = 150 MPa |
- Weld regions:
| fw = z * Rm/3.5 = 0.7 * 525 / 3.5 = 105 MPa |
- Peak regions:
| fp = 1.5 * fg = 1.5 * 150 = 225 MPa |
- Peak/Weld regions:
| fpw = 1.5 * fw = 1.5 * 105 = 157 MPa
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Type of Solution:
Units: Length [mm]; Force [N]; Stress/Pressure [Mpa]
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CONCLUSION:
Vessel
The general stresses in the vessel are well below the acceptable values.
The stresses in the mentioned local regions are more critical.
The analysis shows a significant difference between the Von Mises equivalent stress
and the CODAP stress for several of this local regions.
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Regions of concern for the vessel |
The stresses (both Von Mises and CODAP) at the detector support openings at the end
cover side and in the middle are below 50 MPa (see D in fig). Increasing the stiffness
of the big side opening related to the connection of the hood would only influence
the stresses for the middle detector support opening. Though, the acceptable stress levels give
sufficient margin against a possible underestimate of the stresses.
The stresses at the detector support openings on the exit foil side and the stresses at the
flanges on top of the vessel at the exit foil side (see C and A in fig) are close to acceptable
values for non-localized effects. The Von Mises stresses are close to 100 MPa, the CODAP stresses are
below 50 MPa in the same region. Taking into account these are localized regions the acceptable stress
would be 157 MPa. The stresses are well below the acceptable stresses for localized regions allowing
sufficient safety against possible underestimates of the stresses in these regions due to model errors.
Some stress peaks in the region between the big side openings and the end flanges (see B in fig)
are above the normally accepted values. These values are however acceptable given the fact that the stresses
are compressive, and lay in a transition region of the model where the effects of fillets are not taken
into account.
The buckling factor is 16, where a factor larger than 3 is required. From the stress analysis point of view,
the simulation at the given load (load factor of 1) shows that in the buckling region no plastic deformation occurs.
End cover
The model for the end cover is relatively simple. The main difficulty is the stiffness difference
at the connection between the connection flange of the vessel and the end cover.
The maximum equivalent stress according to Von Mises is 83 MPa and the maximum equivalent stress according to CODAP is 45 MPa.
Both values allow sufficient margin with respect to the acceptable stress of 105 MPa.
The calculated buckling factor is 108, much higher than the required factor 3.
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