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8/18/2019 Wang 2016
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investigate the failure mode and shear buckling strength of the web-
post. An empirical formula which predicted the ultimate vertical shear
buckling strength of web-posts was formulated for the particular web
opening shapes. Lawson, et al. [14] presented simplied equations for
web-post buckling based on strut model, which was calibrated against
results of nite element analyses. Under vertical shear force, the web-
post buckled inan “S ” shape. Hence, it was discordant to check its stabil-
ity using the column buckling curves. And the benecial effect of thein-
clined tension zone was not included in the design.
As shown in Fig. 1(b), it was much reasonable to check the stability
of the web-post based on the plate shear buckling theory. Redwood and
Demirdjian [15] investigated buckling behavior of the web-post in the
CSB with hexagonal openings through studying the upper part of the
web-post under horizontal shear force, as shown in Fig. 2. The horizon-
tal shear buckling strength, V h,cr, of the free body was calculated by
V h;cr ¼ k Eetw
h0=twð Þ2
ð1Þ
where k was the shear buckling coef cient of the upper part of theweb-
post under horizontal shear force. E was the Young's modulus of steel. e
was the width of web-post. t w was the web-post thickness. h0 was the
height of web opening. From the force equilibrium of the free bodyshown in Fig. 2, the vertical shear buckling strength of the web-post
was calculated by
V cr ¼ h−2yi
s V h;cr ð2Þ
where h was the section height of CSB. yi was the distance from the
ange to the centroid of Tee-section. s was the distance between two
adjacent web openings. The buckling strength of the web-post could
be easily determined if k was provided. However, Redwood and
Demirdjian [15] only presented curves to calculate the shear buckling
coef cient k of the web-post with limited geometric parameters.
Substitute Eq. (1) into Eq. (2), the vertical shear buckling strength of
the web-post can be obtained by
V cr ¼ k h−2yi
s
Eetw
h0=twð Þ2
ð3Þ
In this paper, after obtaining the vertical shear buckling strength of
the web-post through FEM simulation, the shear buckling coef cient k
was calculated through reverse analysis. And then an equation was
Fig. 1. Strut inthe web-post. (a) Inclined compressionstrut. (b) Compressionand tension
eld.
Fig. 2. Free body in the CSB with polygonal web openings.
Fig. 3. Conguration of studied CSB.
Fig. 4. FEM of the CSB with hexagonal web openings . (a) Mesh of the CSB with
hexagonal web openings. (b) Load and boundary conditions of the CSB with hexagonal
web openings.
174 P. Wang et al. / Journal of Constructional Steel Research 121 (2016) 173–184
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proposed to calculate k based on the parameter study results. Studies in
this paper followed four steps:
(1) A Finite Element Model (FEM) was proposed and veried by
available test results [10,15,19,20] on CSBs failed in web-post
buckling;
(2) Shear buckling strengths calculated by hand calculated method
proposed by Redwood and Demirdjian [15] were compared
with the FEM simulation results to show its precision;
(3) Parameters affected the shear buckling coef cient k of the web-
post were studied; and then an equation to calculate k was
proposed;
(4) The vertical shear buckling strength of the web-post obtained
using the proposed buckling coef cient k was veried by FEM
and test results [15,19].
2. Finite element model and verication
2.1. Model description and constitutive model of FEM
The CSB was made of Q345 steel with yield strength of 345 MPa and
Poisson's ratio of 0.3. The material behavior provided by ABAQUS [16]
using the PLASTIC option allows a nonlinear stress–strain curve to be
Fig. 5. Comparison of load-middle span deection curves and buckling deformations. (a) Dimension of test beams [10]. (b) Load-middle span deection curves. (c) Bucklingdeformations.
Table 1
Tested CSBs with hexagonal openings [15,19].
Specimens h
(mm)
bf (mm)
t w(mm)
t f (mm)
e
(mm)
h0(mm)
b
(mm)
n L
(mm)
f yw(MPa)
f yf (MPa)
10-5a [15] 380.5 66.9 3.56 4.59 77.8 266.2 76.2 4 1220 352.9 345.6
10-5b [15] 380.5 66.9 3.56 4.59 77.8 266.2 76.2 4 1220 352.9 345.6
10-6 [15] 380.5 66.9 3.56 4.59 77.8 266.2 76.2 6 1828 352.9 345.6
10-7 [15] 380.5 66.9 3.56 4.59 77.8 266.2 76.2 8 2438 352.9 345.6
10-1 [19] 370.59 69.09 3.58 4.39 58.17 245.87 69.85 12 3048 357.1 342
10-3 [19] 376.43 70.61 3.61 4.45 57.91 260.53 127 8 3048 357.1 342
12-1 [19] 476.25 78.49 4.69 5.33 73.41 352.81 101.6 8 3048 311.6 307
12-3 [19] 449.58 78.23 4.62 5.35 71.37 302.51 149.35 6 3048 311.6 307
175P. Wang et al. / Journal of Constructional Steel Research 121 (2016) 173–184
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used. The rst part of the nonlinear curve represents the elastic part up
to the proportional limit stress with Young's modulus of 205 GPa. Since
the non-linear buckling analysis involved large inelastic strains, the
nominal stress–strain curves were converted to true stress and
logarithmic plastic true strain curves. The steel constitutive model in
the proposed FEM used Von Mises yield surfaces with associated plastic
ow, which allowed for isotropic yield. The Von Mises yield surface wasdened by giving the value of the uniaxial yield stress as a function of
uniaxial equivalent plastic strain [17,18].
The studied CSB had four openings along the beam, as shown in
Fig. 3. The vertical concentrated force was applied at the middle span
of the beam. The width and thickness of the two anges were
180 mm and 20 mm, respectively. α was the incline angle of web
Fig. 6. CSB with hexagonal openings [15,19].
Table 2
Shear buckling strengths of CSBs with hexagonal openings obtained from FEM and tests.
Specimens V cr,TEST(kN)
V cr,FEM(kN)
V cr,TEST/ V cr,FEM
10-5a [15] 46.35 45.75 1.05
10-5b [15] 50.45 45.75 1.10
10-6 [15] 47.4 45.75 1.03
10-7 [15] 42.2 41.75 1.01
10-1 [19] 39.55 38.75 1.02
10-3 [19] 36.92 40.64 0.91
12-1 [19] 57.33 58.43 0.98
12-3 [19] 58.22 61.21 0.95
Fig. 7. Comparison of web-post buckling deformations. (a) Test results [19]. (b) FEM
results.
Fig. 8. CSB with cellular openings [20].
Table 3
Test specimen NPI_240 and NPI_280 [20].
Specimens h
(mm)
bf (mm)
t w(mm)
t f (mm)
e
(mm)
h0(mm)
L
(mm)
f yw(MPa)
f yf (MPa)
NPI_240 355.6 106 8.7 13.1 94 251 2846 390 390
NPI_280 406.9 119 10.1 15.2 163 271 2820 290 290
Table 4
Shear buckling strengths of CSBs with circular openings obtained from FEM and tests.
Specimens V cr,TEST [20]
(kN)
Mean value
(kN)
V cr,FEM(kN)
V cr,TEST/ V cr,FEM
NPI_240 Test3 142.05 142.58 152.62 0.93
NPI_240 Test4 143.1
NPI_280 Test1 188.8 187.89 176.81 1.06
NPI_280 Test2 192.1
NPI_280 Test3 186.2
NPI_280 Test4 184.45
Table 5
Comparison of deection obtained from FEM and tests [20].
Specimens wTEST(mm)
Mean value
(kN)
wFEM(mm)
wTEST/ wFEM
NPI_240 Test3 13.892 14.019 15.91 0.88
NPI_240 Test4 14.146
NPI_280 Test1 20.181 20.143 20.036 1.01
NPI_280 Test2 20.694
NPI_280 Test3 19.805
NPI_280 Test4 19.891
Fig. 9. Shearbuckling coef cient forweb-postproposedby Redwoodand Demirdjian [15].
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Fig. 10. Values of k obtained from FEM and proposed by Redwood and Demirdjian [15]. (a) Effects of t w on k, (b) effects of h0/ h on k, and (c) effects of e/ t w on k.
Table 6
Dimensions of web-post to study effects of t w on k.
Group No. e/ t w h0/ e h0/ h t w (mm) e (mm) h0(mm) h (mm)
1
20 3, 4, 5, 6, 7, 8 0.74
6.0 120 360, 480, 600, 720, 840, 960, 480, 640, 800, 960, 1120, 1280
2 8.0 160 480, 640, 800, 960, 1120, 1280 640, 853, 1066, 1280, 1493, 1706
3 10.0 200 600, 800, 1000, 1200, 1400, 1600 800, 1066, 1333, 1600, 1866, 2133
Table 7
Dimensions of web-post to study effects of h0/ h on k.
Group no. e/ t w h0/ e h0/ h t w (mm) e (mm) h0 (mm) h (mm)
120 3, 4, 5, 6, 7, 8
0.746.0
1 20 3 60 , 48 0, 6 00, 7 20, 84 0, 9 60 48 0, 6 40 , 80 0, 96 0, 1 12 0, 12 80
4 0.51 120 360, 480, 600, 720, 840, 960 720, 960, 1200, 1440, 1680, 1920
Table 8
Dimensions of web-post to study effects of e/ t w on k.
Group no. e/ t w h0/ e h0/ h t w (mm) e (mm) h0 (mm) h (mm)
1 203, 4, 5, 6, 7, 8 0.74 6.0
12 0 3 60 , 48 0, 60 0, 7 20 , 84 0, 96 0, 4 80 , 64 0, 8 00 , 9 60 , 11 20 , 1 28 0
5 15 90 270, 360, 450, 540, 630, 720 480, 600, 720, 840, 960
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opening edge. hf was the web height of the Tee-section above the web
opening. l was the half spanof the CSB. t f was the thicknessof theange.
h and bf were the section height and ange width of the CSB.
2.2. Boundary conditions
For the symmetry of the model, only half of the beam was modeled,
asshown in Fig. 4(a). Displacements in y (Uy) and z (Uz)direction of the
bottom ange at the left end of the beam were restrained to simulate
the pin support. The Uz at the top ange was restrained to simulate
the lateral brace. At the right end of the beam, the displacement in x
(Ux) direction and the rotation around y-axis (URy) of theweb were re-
strained. The Uz was also restrained to prevent the beam from failing at
thelateral torsionalbuckling. Forthe top andbottomanges,the Ux and
rotation around z-axis (URz) were restrained. The vertical shear force
was applied at the bottom ange, as shown in Fig. 4(b).
The beam was meshed using the shell element S4R in ABAQUS, a 4-
node quadrilateral shell element with reduced integration and a large-strain formulation, with mesh size of 10 × 10 mm. Theeigenvalue buck-
ling analysis was employed to obtain the elastic buckling strength and
the buckling modes of the web-post.
2.3. Model veri cation
Test results on CSBs with cellular openings by Tsavdaridis and
D'Mello [10], on CSBs with hexagonal openings by Redwood and
Demirdjian [15] and by Zaarour and Redwood [19], and on CSBs with
cellular openings by Erdal and Saka [20] were used to validate the pro-
posed FEM. The beams selected all failed in web-post buckling.
CSBs with cellular web openings tested by Tsavdaridis and D'Mello
[10] were made of UB457 × 152 × 52 and had steel grade of S355, asshown in Fig. 5(a). The yield strength equaled to 375.3 MPa and
359.7 MPa for the web and the anges, respectively; and the ultimate
stresses of the web and the anges were 492.7 MPa and 480.9 MPa, re-
spectively. Thesimply supported beam was loadedat mid-span through
a hydraulic jack. The load-middle span deection curves and failure
modes obtained from FEM agreed well with those from tests, as
shown in Fig. 5(b). The shear buckling strengths of tested specimen
A1 and B1 obtained from test were 133.3 kN and 101.5 kN, respectively,
which were half of the applied concentrated load. The V cr,TEST/ V cr,FEMwere only 0.99 and 1.05 for the two tested beams, respectively. V cr,TESTand V cr,FEM were the shear buckling strengths obtained from test and
FEM, respectively. Failure modes and buckling deformations obtained
from FEM and test all buckled in “S ” shape, as shown in Fig. 5(c),
which proved the validity of the FEM.Test results on CSBs with hexagonal openings carried out by Red-
wood and Demirdjian [15] and Zaarour and Redwood [19] were com-
pared with the FEM results. The tested CSBs were simply supported
and were loaded by a concentrated force at middle span. Vertical stiff-
eners were applied at the two supports and the loading point at the
middle span. Dimensions of tested beams and yield strengths of the
web ( f yw) and the anges ( f yf ) were listed in Table 1. h was the section
height of the CSB. h0 was the height of web opening. bf and t f were the
width and thickness of the ange, respectively. t w was the thickness of
the web. e was the width of web-post. b was the horizontal length of
Table 9
Parameters of CSBs for studying effects of e/ t w.
Group no. Incline angle
α
e/ t w h0/ t w hf / t w t w (mm) e (mm) h0 (mm) hf (mm)
Group I 60° 10, 15, 20, 25, 30, 35, 40, 45, 50, 55, 60 80 15 8.0 80, 120, 160, 200, 240, 280, 320, 360, 400, 440, 480 640 120
Group II 10.0 100, 150, 200, 250, 300, 350, 400, 450, 500, 550, 600 800 150
Group III 12.0 120, 180, 240, 300, 360, 420, 480, 540, 600, 660, 720 960 180
Table 10
Parameters of CSBs for studying effects of h0/ t w.
Group no. Incline angel
α
e/ t w h0/ t w hf / t w t w (mm) e (mm) h0 (mm) hf (mm)
G ro up I V 60 ° 15 40 , 50 , 60 , 70 , 80 , 90 , 10 0, 1 10, 1 20,
130, 140
15 3.0 45 120, 150, 180, 210, 240, 270, 300, 330, 360, 390, 420 45
Group V 6.0 90 240, 300, 360, 420, 480, 540, 600, 660, 720, 780, 840 90
Group VI 10.0 150 400, 500, 600, 700, 800, 900, 1000, 1100, 1200, 1300, 1400 150
Table 11
Parameters of CSBs for studying effects of hf / t w.
Group no. Incline angle
α
e/ t w h0/ t w hf / t w t w (mm) e (mm) h0 (mm) hf (mm)
Group VII 60° 15 80 3, 5, 7, 9, 11, 13, 15, 17, 19, 21, 23 8.0 120 640 24, 40, 56, 72, 88, 104, 120, 136, 152, 168, 184
Group VIII 10.0 150 800 30, 50, 70, 90, 110, 130, 150, 170, 190, 210, 230
Group IX 12.0 180 960 36, 60, 84, 108, 132, 156, 180, 204, 228, 252, 276
Table 12
Parameters of CSBs for studying effects of t w.
Group
no.
Degrees
α
e/ t w h0/ t w hf / t w t w (mm) e (mm) h0 (mm) hf (mm)
Group X 60° 15 80 15 3.0, 4.0, 5.0 ,6.0,
7.0,8.0, 9.0, 10.0, 11.0
45, 60, 75, 90, 105, 120, 135, 150, 165 240, 320, 400, 480, 560,
640, 720, 800, 880
45, 60, 75, 90, 105, 120,
135, 150, 165Group XI 20 60, 80, 100, 120, 140, 160, 180, 200, 220
Group XII 30 90, 120, 150, 180, 210, 240, 270, 300, 330
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Table 13
Parameters of CSBs for studying effects of α .
Group no. Incline angel
α
Tangent value e/ t w h0/ t w hf / t w t w (mm) e (mm) h0 (mm) hf (mm)
Group XIII 85°, 80°, 75°, 70°, 65°, 60°, 55°, 50° 11.43, 5.67, 3.73, 2.14, 1.73, 1.43, 1.20 15 80 15 6.0 90 480 90
Group XIV 8.0 120 640 120
Group XV 10.0 150 800 150
Fig.11. Effectsof web-post dimensionson vertical shearbucklingstrengthof the web-post. (a)Effectsof e/ t w onshearbucklingstrength, (b)effects of h0/ t w on shearbuckling strength,
(c) effects of hf / t w on shear buckling strength, (d) effects of t w on shear buckling strength, and (e) effects of α on shear buckling strength.
179P. Wang et al. / Journal of Constructional Steel Research 121 (2016) 173–184
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the opening edge. L wasthelength of the beam, as shown in Fig. 6. n was
the number of openings of the CSB.
Shear buckling strengths obtained from FEM and tests [15,19] were
listed in Table 2. It could be seen that the shear buckling strengths pre-
dicted by FEM agreed well with those measured from tests [15,19]. The
V cr,TEST/ V cr,FEM variedfrom0.91and 1.05 of theeight beams with a mean
value of 0.99 and a standard deviation of 0.0572.
For beam 10-5a and 10-5b [15], shear buckling deformations of the
web-post obtained from FEM and test were shown in Fig. 7. The FEMand test results both demonstrated that the web-post buckled in “S ”
shape.
Erdal and Saka [20] carried out experiment on cellular steel beams.
Test results of specimen NPI_240 and NPI_280 which failed in web-post
buckling were used to verify the FEM. The cellular steel beams were sup-
portedby round rollers and loaded by a concentrate force at middle span.
Lateral supports were installed at beam ends to prevent the lateral tor-
sional buckling, as shown in Fig. 8. Dimensions of NPI_240 and NPI_280
were listed in Table 3. Shear buckling strengths and vertical deections
obtained from FEM and tests were listed in Tables 4 and 5, respectively.
Results obtained from the FEM with mesh size of 10 mm agreed well
with those measured from tests. The V cr,TEST/ V cr,FEM varied from 0.93
and 1.06 of the six beams with a mean value of 0.99 and a standard devi-
ation of 0.0667. The wTEST/ wFEM varied from 0.88 and 1.01 of the six
beams. wTEST was the deection of the cellular steel beam obtained
from the tests, and wFEM was the deection obtained from FEM.
3. Precision of k proposed by Redwood and Demirdjian [15]
If V cr had been obtained through FEM simulation, the buckling coef-
cient k could be obtained through reverse analysis by
k ¼ V cr h0=twð Þ
2
Eetw
s
h−2yið4Þ
where V cr was the vertical shear buckling strength of the web-post,which could be obtained through FEM eigenvalue analysis.
Thehorizontal shear buckling strength of theweb-post could not ex-
ceed its shear yield strength
V h; p ¼ 0:58etw f y ð5Þ
Substitute Eqs. (2) and (5) into Eq. (4). The corresponding shear
yielding coef cient kp
k p ¼ 0:58 f yE
h0tw
2ð6Þ
Redwood and Demirdjian [15] proposed the shear buckling coef -
cient k as a function of the ratio of web opening height to web-post
width h0/ e, the ratio of web opening height to section height h0/ h, and
the ratio of web-post width to web thickness e/ t w. For h0/ h equaled to
0.51 or 0.74, k could be obtained through Fig. 9 [15]. dg in Fig. 9 [15] rep-
resented section heightof theCSB, which wasdenoted as h in this paper.
Comparison of shear buckling coef cients of web-posts obtained
using the nite element method and method proposed by Redwood
and Demirdjian [15] was shown in Fig. 10(a), (b) and (c). The yield
strength of steel, f y, was 345 MPa. The incline angle of opening edge
was 60°.Effects of web thickness on the shear buckling coef cients of the
web-post were shown in Fig. 10(a). Dimensions of the web-post were
listed in Table 6. Three t w were studied, which were 6.0 mm, 8.0 mm
and 10.0 mm. For theweb-post with thesame e/ t w, h0/ e and h0/ h, k pro-
posed by Redwood and Demirdjian [15] were the same. However, FEM
results showed that k changed with the changes of t w. So it was not
enough to formulate the buckling coef cient by only using thethree di-
mensionless parameters e/ t w, h0/ e and h0/ h. And the k calculated by
Fig. 12. Effects of e/ t w on k.
Fig. 13. Effects of h0/ t w on k.
Fig. 14. Effects of hf / t w on k.
180 P. Wang et al. / Journal of Constructional Steel Research 121 (2016) 173–184
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method proposed by Redwood and Demirdjian [15] was much lower
than that obtained through FEM.
Effects of h0
/ h on the shear buckling coef cients of the web-post
were shown in Fig. 10(b). Dimensions of the web-post studied were
listed in Table 7. Two h0/ h were studied, which were 0.74 and 0.51. Ac-
cording to the curves obtained by Redwood and Demirdjian [15], with
theincrease of h0/ e, the slope ofthe k line with different h0/ h was almost
the same, as shown in Fig. 10(b).However, FEMresults showedthat the
slope of the k line decreased with the increase in h0/ h. k obtained by
Redwood and Demirdjian [15] was still smaller than FEM results.
Effects of e/ t w on k were shown in Fig. 10(c). Dimensions of the web-
post studied were listed in Table 8. Three e/ t w were studied, while t wwas kept constant. k decreased with increase in e/ t w, if it wascalculated
by method presented by Redwood and Demirdjian [15]. FEM results
showed that k nearly kept constant with the increase in e/ t w, if the
web-post had the same t w. k obtained by Redwood and Demirdjian
[15] was smaller than FEM results.
4. Shear buckling strength of web-post
Parameters that affected the buckling behaviors of the web-post
were studied rst to nd out how and to what degrees each parameter
inuenced the V cr. If the vertical shear buckling strength V cr had been
obtained through FEM simulation, then the shear buckling coef cient
k can be calculated by Eq. (4). Then a practical method to calculate k
was proposed based on curve tting of FEM simulation results. And
the vertical shear buckling strength of the web-post was calculated by
Eq. (3) at last.
4.1. Parameters affected vertical shear buckling strength of web-post
CSBs listed in Tables 9–13 were studied to show effects of web-post
dimensions on vertical shear buckling strength of a CSB with hexagonal
webopenings. Analysis results were shown in Fig. 11. Dimensions of the
web-post were represented by dimensionless factors, which were the
ratio of web-post width to web thickness e/ t w, the ratio of web opening
height to web thickness h0/ t w, the ratio of web height of Tee-section
above web opening to web thickness hf / t w, the web thickness t w (in
mm), and the incline angle of web opening edge α .
As shown in Fig. 11(a), (b) and (c), with the increase in e/ t w, h0/ t w
and hf / t w, the shear buckling strength decreased. h0/ t w had great effecton the shear buckling capacity. And with the increase in t w and α , the
shear buckling strength increased, as shown in Fig. 11(d) and (e).
4.2. Effects of geometry parameters on the shear buckling coef cient k
After V cr was obtained through FEM simulation, the buckling coef -
cient k can be obtained by Eq. (4). Parameters that affected k were
investigated through FEM.
4.2.1. Effects of e/t w on k
Three groups of CSBs were studied to show effects of e/ t w on k. Pa-
rameters of the studied CSBs were listed in Table 9. As shown in
Fig. 12, k decreased non-linearly with the increase in e/ t w and it could
be expressed by an exponent function with negative index.
Fig. 16. Effects of α on k.
Fig. 17. Distribution of k obtained from proposed method and FEM.
Table 14
Statistics of (kCAL − kFEM)/ kFEM.
Statistics project Value
Mean 0.004653
Standard error 0.002179
Median 0.000391
Standard deviation 0.027217
Sample variance 0.000741
Minimum −0.043890
Maximum 0.1183996
Sum 0.6978705
Count 150
Fig. 15. Effects of t w on k.
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4.2.2. Effects of h0 /t w on k
Totally 33 CSBs listed in Table 10 were studied to show ef-
fects of h0/ t w on k. As shown in Fig. 13, k increased linearly
with the increase in h0/ t w and it could be formulated by a linear
function.
4.2.3. Effects of h f /t w on k
33 CSBs were studied to illustrate effects of h f / t w on k . Dimen-
sions of CSBs studied were listed in Table 11. As shown in Fig. 14,
k decreased non-linearly with the increase in hf / t w and it could
be formulated by an exponential function.
Fig. 18.Comparisonsof V cr obtained by proposed methodand FEM. (a)Vertical shear buckling strengthof web-post with different e/ t w, (b)vertical shear buckling strength ofweb-post
with different h0/ t w, (c)vertical shear bucklingstrengthof web-post with different hf / t w, (d)vertical shear buckling strength of web-post with different t w, and(e) vertical shear buckling
strength of web-post with different.
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4.2.4. Effects of t w on k
As listed in Table 12, 27 CSBs were studied to show effects of t w on k.
As shown in Fig. 15, k decreased linearly with the increase in t w. It could
also be expressed by a linear function.
4.2.5. Effects of α on k
As listed in Table 13, 24 CSBs were studied to show effects of α on k.
α was represented by its tangent value tan(α ).As shown in Fig. 16, k in-
creased linearly with the increase in tan α . It could also be expressed by
a linear function.
4.3. Practical equations for calculating shear buckling coef cient
Parameter studies showed that k decreased non-linearly with the in-
crease in e/ t w and hf / t w, asshownin Figs. 12 and 14. It increased linearly
with the increase in α and h0/ t w, as shown in Figs. 16 and 13. It de-
creased linearly with t w (in mm), as shown in Fig. 15. As results of nu-
merical regression analysis, k could be calculated by
k ¼ k1 k2 k3 k4 k5≤k p ð7Þ
where
k1 ¼ 0:782 þ 19:712 e
tw
−1:011
ð8Þ
k2 ¼ 0:0325 þ 0:00292h0tw
ð9Þ
k3 ¼ 0:275 þ 0:239exp −0:093h f =twð Þ ð10Þ
k4 ¼ 16:998−0:312tw ð11Þ
k5 ¼ 2:037 þ 0:0360tanα ð12Þ
Comparisons of k obtained from FEM and Eq. (7) were shown in
Figs. 12–16. k obtained by Eq. (7) agreed well with FEM results. Fig. 17
showed differences between k obtained by Eq. (7) and FEM. The differ-
ences were mainly within ±5%, which showed that Eq. (7) could give
accurate predictions on shear buckling coef cient. Here, kCAL was ob-tained by Eq. (7) and kFEM was obtained from FEM analyses. Statistics
of (kCAL − kFEM)/ kFEM were listed in Table 14. The mean value was
only 0.004653 and the standard error was only 0.002179.
4.4. Veri cation
The vertical shear buckling strength of the web-post in a CSB was
predicted by Eq. (3), where k was calculated by Eq. (7). Comparisons
of V cr obtained by Eq. (3) and FEM analysis were shown in Fig. 18. It
could be seen that, for CSBs listed in Tables 9–13, V cr obtained byEq. (3) agreed well with FEM analyses.
Test results on CSBs with hexagonal openings [15,19] were used to
validate the proposed method. Calculated parameters of CSBs were
listed in Table 15. Buckling coef cients k1 ~ k5 and shear buckling
strengths of CSBs obtained from the proposed method and test were
listed in Table 16. The average of (V cr,CAL − V cr,TEST)/ V cr,TEST was 19.7%.
Web-posts in specimen 10-5a, 10-5b,10-6 and 10-7 buckled in theelas-
tic state;and those in specimen 10-1, 10-3, 12-1 and12-3 failed in shear
yielding. For the proposed method was based on the elastic buckling of
the web-post, it overestimated the shear buckling strength when the
web-post buckled in the elastic–plastic state, such as those with thick
web thickness. Through introducing a safety factor of 1.2, the precision
of the proposed method was increased. The average of ( V cr,CAL /1.2 −
V cr,TEST)/ V cr,TEST was reduced to −0.22%, as listed in Table 16.
5. Conclusions
Elastic buckling behaviors of the web-post in the CSB under vertical
shear were investigated using nite element method. Through treating
the upper part of the web-post as a free body under horizontal shear
force, whose shear buckling strength can be calculated by the thin-
plate shear buckling theory, the vertical shear buckling strength of the
web-post was obtained after providing the shear buckling coef cient k.
The shear buckling coef cient k wasnot only affected by thedimen-
sionless parameters of the web-post, such as e/ t w, h0/ t w, and hf / t w, but
also the thickness of the web-post t w and incline angle of the opening
edge α . k was calculated through reverse analysis after the vertical
shear buckling strength of the CSB was obtained through FEM simula-tion. e/ t w, h0/ t w, and h f / t w, t w and α all had great inuences on the
shear buckling coef cient. A simplied method was proposed to calcu-
late k. The vertical shear buckling strength of the web-post employing
the proposed k agreed well with FEM results.
For the proposed method was based on the elastic buckling of the
web-post, it overestimated the shear buckling strength when the
web-post buckled in the elastic–plastic state, such as those with thick
web thickness. The average of (V cr,CAL − V cr,TEST)/ V cr,TEST was 19.7%.
Through introducing a safety factor of 1.2, the precision of the proposed
method was increased. The average of (V cr,CAL /1.2 − V cr,TEST)/ V cr,TESTwas reduced to −0.22%. The simplied method for calculating shear
buckling coef cient k in elastic–plastic state needed to be investigated
later.
The proposed equation for calculating the shear buckling strength of web-posts was derived from the CSBs with hexagonal web openings.
Table 16
Shear buckling strength of CSBs obtained by proposed method and tests [15,19].
Specimens k1 k2 k3 k4 k5 kp k V cr P TEST (kN) (V cr,CAL − V cr,TEST)/ V cr,TEST (V cr,CAL /1.2 − V cr,TEST)/ V cr,TEST
10-5a [15] 1.65 0.25 0.34 15.89 2.10 5.58 4.64 54.23 46.35 17.0% −2.5%
10-5b [15] 1.65 0.25 0.34 15.89 2.10 5.58 4.64 54.23 50.45 7.5% −10.4%
10-6 [15] 1.65 0.25 0.34 15.89 2.10 5.58 4.64 54.23 47.4 14.4% −4.7%
10-7 [15] 1.65 0.25 0.34 15.89 2.10 5.58 4.64 54.23 42.2 28.5% 7.1%
10-1 [19] 1.96 0.23 0.33 15.88 2.10 4.77 4.99 57.42 39.55 45.2% 21.0%
10-3 [19] 1.97 0.24 0.34 15.87 2.07 5.26 5.30 40.97 36.92 11.0% −7.5%
12-1 [19] 2.00 0.25 0.35 15.53 2.10 4.99 5.82 79.47 57.33 38.6% 15.5%
12-3 [19] 2.02 0.22 0.34 15.56 2.07 3.78 4.89 55.71 58.22 −4.3% −20.3%
Average 21.0% 0.8%
Table 15
Calculated parameters of CSBs with hexagonal web openings.
Specimens e/ t w h0/ t w hf hf / t w t w α tanα yi s (mm)
10-5a [15] 21.85 74.78 52.56 14.76 3.56 60.00 1.73 13.11 308.00
10-5b [15] 21.85 74.78 52.56 14.76 3.56 60.00 1.73 13.11 308.00
10-6 [15] 21.85 74.78 52.56 14.76 3.56 60.00 1.73 13.11 308.00
10-7 [15] 21.85 74.78 52.56 14.76 3.56 60.00 1.73 13.11 308.00
10-1 [19] 16.25 68.68 57.97 16.19 3.58 60.00 1.73 14.86 256.04
10-3 [19] 16.04 72.17 53.50 14.82 3.61 45.00 1.00 13.26 369.82
12-1 [19] 15.65 75.23 56.39 12.02 4.69 60.00 1.73 14.62 350.0212-3 [19] 15.45 65.48 68.19 14.76 4.62 45.00 1.00 18.46 441.44
183P. Wang et al. / Journal of Constructional Steel Research 121 (2016) 173–184
8/18/2019 Wang 2016
12/12
Whether the CSBs with other web opening shapes could use the pro-
posed equation needed to be investigated later.
Acknowledgments
Theauthors wish to acknowledge thesupport from theFundamental
Research Funds of Shandong University (No. 2015JC 046), the Natural
Science Foundation of Shandong Province (ZR2015EM041) and the Nat-
ural Science Foundation of China (51578322) for the work reported inthis paper.
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