Copyright Prentice-Hall Chapter 16 Sheet-Metal Forming Processes.
Metal Structures Design Project III Steel hall examples of ...
Transcript of Metal Structures Design Project III Steel hall examples of ...
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Metal Structures
Design Project III
Steel hall – examples of calculation (part I)
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Ist example of calculations – continous suspended cold-formed purlin
Photo: kingspan.com
Photo: Author
Dead-weigth of purlin is at now probably smaller (cold-formed is lighter than hot rolled).
But participation of dead-weight in total load (max part = snow) is small, and difference
between hot rolled and cold-formed is completely neglegible in comparison to total load.
For calculation could be taken completely the same value of load as for purlins in Ist desig
project.
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yPhoto: Author
z
qz = 12,217 kN/m
qy = 0,960 kN/m
qy = qy[qH(s)] + qy[qV(s)] + qy[qH(g)] + qy[qV(g)] + qy(w) =
= 0,000 + 0,872 + 0,000 + 0,088 + 0,000 = 0,960 kN / m
qz = qz[qH(s)] + qz[qV(s)] + qz[qH(g)] + qz[qV(g)] + qz(w) =
= 0,000 + 9,962 + 0,000 + 1,000 + 1,255 = 12,217 kN / m
MEd, y = qz L2 / 8 = 54,977 kNm
MEd, z = qy L2 / 8 = 4,320 kNm
VEd, y = qy L / 2 = 2,880 kN
VEd, z = qz L / 2 = 36,651 kN
→ Des #1 examp / 10
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Photo: Author
Continous multispan purlin could be calculated with using of table for calculations.
Results for 2- , 3- , 4- and 5-span bealm are presented in table. For 6- and more span we can use
information for 5-span beam.
First span
First span
Second span
Second span
Last span
Last span
Penultimate span
Penultimate span
Central span
Central span many times
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Photo: Tablice do projektowania
konstrukcji metalowych, W.
Bogucki, M. Żyburtowicz, Arkady
1996 Warszawa
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Photo: Tablice do projektowania konstrukcji metalowych, W. Bogucki,
M. Żyburtowicz, Arkady 1996 Warszawa
Scheme 1: for dead-weight g
Schemes 2-5: for live load q
g(1) + p(2) – max moments M1 , M3 amd reaction A
g(1) + p(3) – max moments M2
g(1) + p(4) – max moments MB and reaction B
g(1) + p(5) – max moments MC and Reaction C
Because of division between dead-wight and live loads, data from #t / 3 must be recalculated
to effects of g and q.
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qH
Photo: Author
qV
s → qH, qV ; l
g → qH, qV ; l1
w → qy, qz ; l1
d1
d
qH(s) = 0,000 kN / m
qV(s) = s d = 10,000 kN / m
qH(g) = 0,000 kN / m
qV(g) = g d1 = 1,004 kN / m
qy(w) = 0,000 kN / m
qz(w) = w d1 = 1,255 kN / m
d1
d
l1 = 2 d1 / 2 = d1
l = 2 d / 2 = d
→ Des #1 examp / 8
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qH
Photo: Author
qV
qH → qy , qz
qV → qy , qz
qy(qH) = qH cos a
qz(qH) = - qH sin a
qy(qV) = qV sin a
qz(qV) = qV cos a
qy[qH(s)] = qH(s) cos a = 0,000 kN / m
qz[qH(s)] = - qH(s) sin a = 0,000 kN / m
qy[qV(s)] = qV(s) sin a = 0,872 kN / m
qz[qV(s)] = qV(s) cos a = 9,962 kN / m
qy[qH(g)] = qH(g) cos a = 0,000 kN / m
qz[qH(g)] = - qH(g) sin a = 0,000 kN / m
qy[qV(g)] = qV(g) sin a = 0,088 kN / m
qz[qV(g)] = qV(g) cos a = 1,000 kN / m
→ Des #1 examp / 9
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Ultimately, information from #t / 3
qz = 12,217 kN/m qy = 0,960 kN/m
and information from #t / 8
qy[qV(g)] = qV(g) sin a = 0,088 kN / m
qz[qV(g)] = qV(g) cos a = 1,000 kN / m
can be presented as
qz = 12,217 kN/m = qz(g) + qz(q) = gz + qz = 1,000 kN / m + 11,217 kN / m
qy = 0,960 kN/m = qy(g) + qy(q) = gy + qy = 0,088 kN / m + 0,872 kN / m
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Photo: Author
Purlin is supported:
• In direction z by main roof girder;
• In direction y by main roof girder and additional suspension for purlins in halg between
girders.
This types of supports make two warious static schemes in both directions.
MEd, y (qz)
MEd, z (qy)
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Photo: Author
MEd, y, max in span MEd, y, max in span MEd, y, max in span
MEd, y, max over support MEd, y, max over support
MEd, z, max over support MEd, z, max over support MEd, z, max over support
MEd, z, max over support MEd, z, max over support
Such type of static scheme makes, that max values MEd, y, max – over supports on in spans –
correspond max values MEd, z, max – only over supports.
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Photo: Author
Information in table about shear forces are presented for left (L) and right (P – prawy) cross-
section nest to support. Reaction R = |QL| + |QP|
QLQP
R
Photo: Author
* * *
Reactions in additional supports in direction y are loads applied to suspension bars.
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Coefficents in direction z:
Point Value g(1) q(2) q(3) q(4) q(5)
A RA 0,395 0,447
1 MEd, y, 1 0,0781 0,1000
B MEd, y, B 0,1050 0,1190
RB 0,556 1,218
2 MEd, y, 2 0,0331 0,0787
C MEd, y, C 0,0789 0,1110
RC 0,979 1,167
3 MEd, y, 3 0,0462 0,0855
A B C
1 2 3
Photo: Author
Ri = agi, R g L + aqi, R q L
Mi = agi, M g L2 + aqi, M q L2
L = 6m
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Values:Point Value
A RA 32,454 kN
1 MEd, y, 1 43,193 kNm
B MEd, y, B 51,834 kNm
RB 85,310 kN
2 MEd, y, 2 32,971 kNm
C MEd, y, C 47,664 kNm
RC 84,415 kN
3 MEd, y, 3 36,189 kNm
A B C
1 2 3
Photo: Author
Max M over support
Max M in span
Max R
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Cold-formed Z-purlins are often joined over support by overlap. Resistance abowe
support is abut two times bigger than in span.
Photo: ruukki.com
Photo: forminometal.com
Because of this, fo calculation important is
only bending moment in span.
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Point Value
A RA 32,454 kN
1 MEd, y, 1 43,193 kNm
B MEd, y, B 51,834 kNm
RB 85,310 kN
2 MEd, y, 2 32,971 kNm
C MEd, y, C 47,664 kNm
RC 84,415 kN
3 MEd, y, 3 36,189 kNm
A B C
1 2 3
Photo: Author
A B C C C C
Direction z
Direction y
Bending moment MEd, y in span 3
corresponds bending moment MEd, z
over support C.
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Point Value L = 3 m No suspension, L = 6 m (for comparison)
A RA 1,274 kN 2,548 kN
1 MEd, y, 1 0,847 kNm 3,388 kNm
B MEd, y, B 1,017 kNm 4,068 kNm
RB 3,333 kN 6,667 kN
2 MEd, y, 2 0,642 kNm 2,568 kNm
C MEd, y, C 0,934 kNm 3,736 kNm
RC 3,311 kN 6,622 kN
3 MEd, y, 3 0,708 kNm 2,832 kNm
1 2 3
Photo: Author
A B C C C C
Direction y
3 3 3L = 3m
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Photo: Author
Resistance of purlin could be analised in main central
axes x h or in axes y z paralell to web and flange.
y
a
b
x
h
a
z
No cooperation between purlin and
housing (for example: after many years
post erection of structure complex of
small destructions in bolts, purlins and
housing eliminates cooperation).
Cooperation between purlin and
housing (through ~ 10 years since
erecton of structure).
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Calculations in axes y-x:
Z 400-3:
Wy = 180,34 cm3
Wz = 19,02 cm3
Vertical part of web = (40 – 2 ∙ 1,5 ∙ 0,3) ∙ 0,3 = 11,73 cm2
Horizontal part of flages = 2 ∙ (8,5 – 2 ∙ 1,5 ∙ 0,3) ∙ 0,3 = 4,56 cm2
Photo: pruszynski.com.pl
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sy = MEd, y / Wy + MED, z / Wz = 200,627 MPa + 47,124 MPa = 247,124 MPa
ty = Vy / Avy = 7, 309 MPa
tz = Vz / Avz = 72,728 MPa
EN 1993-1-1 (6.1):
S235:
[sy / (fy gM0)]2 + 3 [(tz
2 + tz2) / (fy gM0)
2] = 1,18 > 1,0 wrong
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Deflections:
Value of deflections can be approximated by one of two ways:
• Values from „normal” static calculations;
• Values from formula:
D = 0,50 [5 g L4 / (384 E J)] + 0,75 [5 q L4 / (384 E J)]
where
D - deflection; g – dead weight; q – live load; L – length of one span
→ Proj #2 / 28
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According to #t / 9:gz + qz = 1,000 kN / m + 11,217 kN / m
According to #t / 19:Jy = 3653,93 cm4
Dz = 0,50 [5 gz L4 / (384 E Jy)] + 0,75 [5 qz L4 / (384 E Jy)] = 0,020 m
Dacc (#11 / 94) = L / 200 = 0,030 m
Dz / Dacc = 0,667 < 1 OK
Photo: Author
Suspension makes, that max Dz corresponds with Dy = 0. Dy is neglegible.
Dz
Dy
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Reactions in additional supports in direction y are loads applied to suspension bars (#t / 12).
According to #t / 17, this force = 3,333 kN.
Round bar F 8mm; A = 0,503 cm2
Nt,Rd = A fy / gM0 = 11,812 kN
F / Nt,Rd = 0,282 < OK
Compression in suspended bars is not taken into consideration. Such slenderness members losts
stability under even small compressive force.
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Photo: A. Biegus, Przyczyny przedawaryjnego stanu technicznego płatwi
hali stalowej, Budownictwo i Architektura 12 / 2013, 173-180
Photo: dromet.pl
Purlin Purlin
Hanger after buckling
There is possible compression in part of hangers. There will be permanently deformations as
the effect of buckling.
We need rigging screws to repair hangers.
→ #8 / 34
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IInd example of calculations – main column in frame
Photo: Author
Forces shoul be applied in point – as
effect of contact with purlins and wall
girts.
For big number of purlins and girts,
loads could be applied as continous.
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Photo: Author
Point A:
Horizontal force = wind action on wall from wall girt + horizontal compoun from wind action
on purlin
Vertical force = dead weight of wall girt + dead weight of housing panels + dead weigth of
purlin + dead weight of roofing panels + snow + vertical compoun from wind action on purlin
Point B:
Horizontal force = wind action on wall from wall girt
Vertical force = dead weight of wall girt + dead weight of housing
Point C:
Horizontal force = horizontal compoun from wind action on purlin
Vertical force = dead weigth of purlin + dead weight of roofing panels + snow + vertical
compoun from wind action on purlin
A
B
CA
B
C
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General notice
Main roof girder is calculated according to the same algorithm, as main column. The same,
resistance, stability and deformation must be taken into consideration.
Resistance is checked completely the same for girger and column.
Stability for girder is calculated for specific critical lengths (→ #10 / 57).
Deformation for girder is vertical deflection of ridge.
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Photo: Author
Columns: HEA 450
H = 5,45 m
Girders: HEA 450
L = 23,50 m
MEd, top = 311,6 kNm
MEd, bottom = 0,0 kNm
NEd, top = 93,4 kN
NEd, bottom = 97,6 kN
VEd, max = 57,2 kNm
Resistance and stability of main columnn
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Single-storey frame
n = 1
Photo: Author
m ≥ 1
Eurocode – N.A.
Experience – general rules
C1
T:
m ≤ 1,0
R
G
F
P
D
R
C
B
A
T:
m =?
m =1
s.i+II
s.b.i
+II
Co:
m =?
Methods:Resistance
Stability:Deformations
Critical length:
→ #13 / 92
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Recommended algorithm for Your design project:
n = 1
Photo: Author
m ≥ 1
R
GDC T:
m =?
*
*
*
*
** * *
*
* * *
*
*
C1
T:
m ≤ 1,0
Co:
m =?
Few additional information (→ #t / 32)
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Procedure "C"
„Normal” loads are taken into consideration only.
Photo: Author → #13 / 53
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„Normal” loads in procedure C means loads from dead-weight, snow, wind, imposed,
thermal, etc. In opposite to method A or B, effects from imperfection and second order
effects are not taken into consideration. Cross-sectional forces for method C are presented
in #t / 28.
In method A or B more combinations of actions are taken into consideration in
comparison to C. But analisis of instability in these two methods is simpler, than in C.
In method C, critical length of column in plane of frame must be calculated.
According to EN 1993-1-1 N.A. 9 (C1 on #t / 30), one-storey steel frame can be calculated
without second order effects and incluences of imperfection and, additionaly, as non-sway
frame. Critical length of column in non-sway frame is not greater than height of column.
If we do not make accurate calculations of m (of course m ≤ 1,0), we can taken into
consideration m = 1,0 , the same as in method B.
Critical length can be calculated by computer (m = ?). More information is presented on
#13 / 69-70. This method is accepted in Your range of project as second method, to
verification results from tables.
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Single-storey frame
"Tablice do projektowania konstrukcji metalowych", W. Bogucki, M. Żyburtowicz, Arkady, Warszawa 1984
(n = m)
→ #13 / 56
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Data for calculation:
h = 5,45 m
b = 23,50 m
F = area of cross-section of column = A (HEA 450) = 98,8 cm2
J0 , J = moments of inertia for cross section of left and right column = J (HEA 450) =
= 33 740 cm4
P0, P1 – equivalent vertical loads from roof; for symmetrical frame P0 = P1
n = P1 / P0 = 1,000000
c = J b / (J0 h) = 4,311927
s = 4 J / (b2 F) = 0,000247
m = {√[0,5(1 + n)]} {√[4+1,4(c + 6s) + 0,02 (c + 6s)2]} = 3,227
Critical length of column in plane of frame is equal:
5,45 m ∙ 3,227 = 17,587 m
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Critical length of column in out-of-plane of frame, because of vertical bracings between
columns, is equal:
5,45 m
The same for critical length foe lateral buckling.
Photo: steelwarehousechina.com
Photo: greenterrahomes.com
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Resistance must be analised in each characteristic point separately. For frame as follow:
In top point of column and in bottom point of column.
Photo: Author
MEd, top = 311,6 kNm
MEd, bottom = 0,0 kNm
NEd, top = 93,4 kN
NEd, bottom = 97,6 kN
VEd, max = 57,2 kNm
Shear force the same should be analised separately for top and bottom poin, but for sch
small value can be analised max value.
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HEA 450 [mm]
h b tf tw r
440 300 21 11,5 27
A = 178,0 cm2
Jy = 63 720 cm4
Jz = 9465 cm4
Wy, pl = 3216 cm3
Wz, pl = 965,5 cm3
AV, z ≈ 92,4 cm2
MRd, y = 755,760 kNm
NRd = 4183,0 kN
VRd = 1253,658 kN
Photo: Author
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Resistance: top point
MEd, top = 311,6 kNm
NEd, top = 93,4 kN
VEd, max = 57,2 kNm
MEd, top / MRd, y = 0,412 < 1,0 OK
NEd, top / NRd = 0,022 < 1,0 OK
VEd, max / VRd = 0,046 < 1,0 OK
VEd, max / VRd = 0,046 < 0,5 → no interaction between shear force and bending moment
min ( 0,25 Npl, Rd ; 0,5 hw tw fy / gM0) = min (1045,750 ; 464,830) = 464,830 kN
NEd, top < 464,830 kN → no interaction between axial force and bending moment
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Resistance: bottom point
MEd, bottom = 0,0 kNm
NEd, bottom = 97,6 kN
VEd, max = 57,2 kNm
MEd, top / MRd, y = 0,0 < 1,0 OK
NEd, top / NRd = 0,023 < 1,0 OK
VEd, max / VRd = 0,046 < 1,0 OK
No bending moment → no interaction with shear force and axial force
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Stability is analised for total member. This means global calculation for maximum values
of NEd, My, Ed, Mz, Ed even if they are in three different cross-sections.
MEd = MEd, top = 311,6 kNm
NEd = NEd, bottom = 97,6 kN
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NEd / ( cy NRk / gM1) + kyy (My, Ed + DMy, Ed ) / ( cLT M y, Rk / gM1) +
+ kyz ( Mz, Ed + DMz, Ed ) / (M z, Rk / gM1) ≤ 1,0
NEd / ( cz NRk / gM1) + kzy (My, Ed + DMy, Ed ) / ( cLT M y, Rk / gM1) +
+ kzz ( Mz, Ed + DMz, Ed ) / (M z, Rk / gM1) ≤ 1,0
kyy , kyz , kzy , kzz
"French" method EN 1993-1-1 App. A, table A1, A2
"German" method EN 1993-1-1 App. B, table B1, B2, B3
"French" and "German" methods:
EN 1993-1-1 (6.61), (6.62)
→ #13 / 77
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Interaction between flexural buckling in plane of frame (Lcr = 17,587 m, buckling about
stron axis of HEA 450) and lateral buckling (Lcr = 5,450 m):
NEd / ( cy NRk / gM1) + kyy (My, Ed + DMy, Ed ) / ( cLT M y, Rk / gM1) +
+ kyz ( Mz, Ed + DMz, Ed ) / (M z, Rk / gM1) ≤ 1,0
Interaction between flexural buckling out of plane of frame (Lcr = 5,450 m, buckling about
weak axis of HEA 450) and lateral buckling (Lcr = 5,450 m):
NEd / ( cz NRk / gM1) + kzy (My, Ed + DMy, Ed ) / ( cLT M y, Rk / gM1) +
+ kzz ( Mz, Ed + DMz, Ed ) / (M z, Rk / gM1) ≤ 1,0
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No bending moment out of plane of truss → Mz, Ed = 0,0 kNm
HEA 450 Ist class of cross section, no diference between global and effective center of
gravity, no eccentricities → ez = 0,0 m ; ey = 0,0 m
DMy, Ed = NEd ez = 0,0 kNm
DMz, Ed = NEd ey = 0,0 kNm
NEd / ( cy NRk / gM1) + kyy My, Ed / ( cLT M y, Rk / gM1) ≤ 1,0
NEd / ( cz NRk / gM1) + kzy My, Ed / ( cLT M y, Rk / gM1) ≤ 1,0
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Flexural buckling, axis y Ncr, y = p2 EJy / (my l0y)2 = 4 269,837 kN
Flexural buckling, axis z Ncr, z = p2 EJz / (mz l0z)2 = 6 604,602 kN
Torsional buckling Ncr, T = [p2 EJw / (mT l0T)2 + GJt] / is2 = 5 446,494 kN
Lateral buckling Mcr = is √ (Ncr, z Ncr, T) = 1793,300 kNm
lLT = √ (Wy, pl fy / Mcr) = 0,649
FLT = 0,684
cLT = min{1/[FLT + √ (FLT2 - lLT
2)] ; 1/ lLT2 ; 1,0} = 1,0
cLT, mod = 1,0
ly = √ (A fy / Ncr, y) = 0,990
Fy = 1,128
cy = 0,599
lz = √ (A fy / Ncr, z) = 0,633
Fz = 1,306
cz = 0,408
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"German" method EN 1993-1-1 tab. B.3
Moment diagram Range Cmy and Cmz and CmLT
Uniform loading Concentrated loading
-1 ≤ Y ≤ 1 max (0,6 + 0,4 Y ; 0,4)
For members with sway buckling mode, the equivalnet uniform moment factor should be taken Cmy = 0,9 or Cmz = 0,9 respectively.
Cmy, Cmz and CmLT should be obtained according to the bending moment between the relevant braced points as follows:
Moment factor: bending axis: points braced in direction:
Cmy y-y z-z
Cmz z-z y-y
CmLT y-y y-y
Y = 0
Cmy = Cmz = CmLT = max (0,6 + 0,4 Y ; 0,4) = 0,6
But „For members with sway buckling mode…” → This is sway
mode of instability for such frame.
Cmy = Cmz = 0,9
CmLT = 0,6Photo: Author
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For "German" method, members are divided into susceptible to torsional deformations and
not susceptible to torsional deformations.
Cross-section Comments
No lateral buckling, no need for buckling
interaction analysis
Member not susceptible to torsional
deformations, EN 1993-1-1 tab. B.1
Member susceptible to torsional
deformations, EN 1993-1-1 tab. B.2
Short member:
1 / [FLT + √ (FLT2 - lLT
2)] ≥ 1,0
1 / [FLT + √ (FLT2 - lLT
2)] < 1,0
kq →
→ #13 / 79
Analised case → Tab B.1
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EN 1993-1-1 tab. B.1
ny = NEd gM1 / (cy NRd )nz = NEd gM1 / (cz NRd )
Interaction
factors
Cross-
section
Ist, IInd class IIIrd, IVth class
kyy I, H, RHS Cmy ∙ min {1 + 0,6 ly ny ;
1 + 0,6 ny}
Cmy ∙ min {1 + (ly – 0,2) ny ;
1 + 0,8 ny}
kyz I, H, RHS 0,6 kzz kzz
kzy I, H, RHS 0,6 kyy 0,8 kyy
kzz I, H Cmz ∙ min {1 + (2 lz - 0,6) nz ;
1 + 1,4 nz} Cmz ∙ min {1 + 0,6 lz nz ;
1 + 0,6 nz}RHS Cmz ∙ min {1 + (lz - 0,2) nz ;
1 + 0,8 nz}
For I- and H-sections and RHS, under axial compression and unaxial bending My, ED, the
coefficient kzy may be = 0
"German" method,
interaction factors→ #13 / 80
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ny = NEd gM1 / (cy NRd ) = 0,038
nz = NEd gM1 / (cz NRd ) = 0,056
Interaction
factors
Cross-
section
Ist, IInd class
kyy I, H, RHS Cmy ∙ min {1 + 0,6 ly ny ;
1 + 0,6 ny} = 0,919
For I- and H-sections and RHS, under axial
compression and unaxial bending My, ED, the
coefficient kzy may be = 0
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NEd / ( cy NRk / gM1) + kyy My, Ed / ( cLT M y, Rk / gM1) ≤ 1,0
NEd / ( cz NRk / gM1) ≤ 1,0
97,6 / (0,599 ∙ 4183,0 / 1,0) + 0,919 ∙ 311,6 / (1,0 ∙ 755,76 / 1,0) = 0,418 ≤ 1,0 OK
97,6 / (0,633 ∙ 4183,0 / 1,0) = 0,037 ≤ 1,0 OK
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Deformation
Horizontal displacement of top point of column:
0,002 m
Accepted value:
H / 150 = 0,036 m
D / Dacc = 0,056 < 1,0 OK