A DESIGN OF (G+4) LOW COST BUILDING AND ITS COST ESTIMATION (BY USING RIBBED SLAB) CHAPTER-ONE ROOF DESIGN Wind load analysis and design Wind is a moving air which in turn possesses energy and this kinetic energy should be resisted by using appropriate deign for different kinds of structural elements like roofs ,walls The action of wind can be a type of suction or pressure to our structures both externally or internally .How ever these effects are more magnified for structure with more openings and large surface areas .And we focus on sensitive part of the building that is roofs (both hipped and flat roofs) for analysis and design of its parts . Method of analysis Even though there are two methods for wind load analysis ,namely Quasi static method and dynamic analysis we prefer Quasi static since our structure is assumed to be less susceptible to dynamic excitation and from EBCS-1,1995 section 3.9.3 a building which satisfies the criterion: (For c d <1.2and building height less than 200m) can be analyzed using Quasi static Roof analysis and design Before going to the direct steps we should classify the location, terrain category our building site. And our building is located at Adigrat and we told that there are buildings around it. And according to External pressure External pressure W e is obtained from: W e =q ref * C e (Z e )*C pe Where C pe - is the external pressure coefficient MEKELLE UNIVERSITY, FACULITY OF SCIENCE AND TECHNOLOGY DEPARMENT OF CIVIL ENG’G 1
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A DESIGN OF (G+4) LOW COST BUILDING AND ITS COST ESTIMATION (BY USING RIBBED SLAB)
CHAPTER-ONE
ROOF DESIGN
Wind load analysis and design Wind is a moving air which in turn possesses energy and this kinetic energy should be resisted by using appropriate deign for different kinds of structural elements like roofs ,walls The action of wind can be a type of suction or pressure to our structures both externally or internally .How ever these effects are more magnified for structure with more openings and large surface areas .And we focus on sensitive part of the building that is roofs (both hipped and flat roofs) for analysis and design of its parts.
Method of analysis Even though there are two methods for wind load analysis ,namely Quasi static method and dynamic analysis we prefer Quasi static since our structure is assumed to be less susceptible to dynamic excitation and from EBCS-1,1995 section 3.9.3 a building which satisfies the criterion: (For cd <1.2and building height less than 200m) can be analyzed using Quasi static
Roof analysis and design Before going to the direct steps we should classify the location, terrain category our building site. And our building is located at Adigrat and we told that there are buildings around it. And according to
External pressure
External pressure We is obtained from: We =qref * Ce(Ze)*C pe
Where Cpe - is the external pressure coefficient Ce(Ze)- is the exposure coefficient qref - is the reference wind pressure
i. Reference wind pressure
This is determined from; qref = 0.5 *ρ*v2
ref
Where ρ is the air density and for an altitude of 1500m (approximate) above sea level. ρ = 1.00 kg /m3 Vref = the reference wind velocity and is given as Vref = CDIR * CTEM * CALT * Vref,0
Taking the three factors as unity and given Vref,0 =22 m/s, finally we get the reference wind pressure to be qref = 0.5 *(1.00 kg/m3) *(22.0 m/s)2
= 242 pa
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ii. External coefficient According to section 3.8.5(2), the exposure coefficient is given by,
Ce(z) =
Where KT –is the terrain factor Cr(z) – is the roughness coefficient Ct(z) – is the topography coefficient and taken to be unity For the terrain classification, the site is assumed to fall under category iv (the worst case) which is urban area in which at least 15% of the surface is cover with buildings and their average height exceeds 15m. Then, from table 3.2, KT = 0.24 , Z0 = 1m , Zmin = 16mThe actual height of the building, Ze, is equal to 16.7m
Cr(Ze)=KT*ln for Zmin Ze 200m
Cr(Ze) = Cr(Zmin) , for Ze Zmin
Where KT- terrain factor Z0 – roughness length Zmin – minimum height Since 16m <16.4m < 200m, we have to use the 1st one. Then; Cr(Ze) = 0.676 , Ct(Ze) =1.0 Ce(Ze) = 1.59 We have two separated and almost typical adjacent buildings, so the computation, analyze and result of one building can be used for the other one.
iii. External pressure coefficient Our roof is considered as both monopitch and hipped roof. The external pressure coefficient depends on the size of the loaded area, A, and as per the code it is given as: Cpe = Cpe, 1 A 1m2
Cpe =Cpe, 1 + (Cpe, 10 – Cpe, 1) log A 1m2 < A < 10m2
Cpe = Cpe,10 A 10m2
Our roof is modeled and designed as both monopitch (according to appendix A.2.4) and hipped roof (according to appendix A.2.6) of EBCS -1 , 1995. Case-1 Wind direction = 0 5.85m 18.27m M 12.06m 5.188m H L 2.412m F1 G F2 2.412m 6.03m 12.06m 6.03m =0
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e = b or 2h which ever is smaller e = min e = 24.12m The pitch angle;
α0 = tan-1 =12.61 Since α0=12.61 applying linear interpolation between +5 +15 the following result is obtained.
Table 1.1 Cpe values for = 0Zone F G H L M
Cpe,10 -1.092 -0.896 -0.372 -1.352 -0.6
-0.256 -0.136 0.008 - -
Cpe,1 -2.12 -1.62 -0.516 -2.0 -0.624
-0.448 -0.328 -0.136 - -
Table 1.2 will gives the Cpe values and their respective wind pressure for the different parts of the roof and the bigger Cpe values is taken for a given roof part.
Table 1.2 wind pressures for =0Zone F1 F2 G H L M
Area(m2) 14.54 12.31 29.09 105.5 14.11 26.839
Cpe -1.092 -1.092 -0.896 -0.372 -1.352 -0.6
-0.256 -0.256 -0.136 +.008 - -
Wind pressure(N/m2
= - 420.18N/m2(suction)= +3.08N/m2(pressure)
= - 520.22N/m2(suction)
Case-2 Wind direction = 90
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4.765m 1.085m F2 2.71m 18.27m H G 5.43m =90 7.6m N L F1 M 2.71m 17.61m 5.425m 1.085m
e = min e = 10.85
And pitch angle 90 = tan-1 = 16.2 Applying linear interpolation between = +15 and +30 for = 16.2 the Cpe values are as follows.
Table 1.3 Cpe values at =90Zone F G H L M NCpe,10 -0.788 -0.776 -0.292 -1.4 -0.616 -0.292
Internal pressure Internal pressure,Wi is the obtained from Wi = qref *Ce(zi) * Cpi
Where Cpi is the internal pressure coefficient and according to the code for closed buildings with internal partitions and opening windows. Cpi = 0.8 or -0.5 Ce(zi) = Ce(ze) =1.59 qref = 242 pa Therefore the extreme values of the internal pressure are Wi = 242 * 1.59 *(0.8) =307.824 pa (pressure) And Wi = 242 * 1.59 *(-0.5) = -192.39 pa (suction) Net pressure
The net wind pressure is the difference of the pressures on each surface taking due account of their signs. And there will be various net wind pressure combinations out of
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which the severe cases are taken. These combinations are determined for purlin design and truss analysis at every step. live load
Since the roof is in accessible except for normal maintenance or other similar things, it follows under category H and accordingly for sloping roof. qk= 0.2 5KN/m2
QK = 1.0KN Dead load
The dead load of the purlin and truss members also determined in the following steps.
- self weight of the roof cover = 130N/m2
- self weight of the ceiling chip board. = 8KN/m3
load combination Combination of actions for persistent and transient design situations is determined according to section 1.9.4.5 of EBCS-1,1995, considering ultimate limit state ,cases to be considered are Case-1 unfavorable = 1.1DL + 1.35(WL (pressure +LL) Case-2 favorable =0.9 DL +1.6 WL (suction)
Truss lay out T2 1.6m T2
1.6m T2
3.8m T3
T1 T1 T1 T1 T1 T1 T1 T1 T1 T4 T5 3.8m
2m 2m 2.5m 2.5m 2m 2m 1.78m 1.78m 2.925m 2.925m
Truss types
TYPE-1(T1) Panel length, s = 1.2979m Pitch angle, =12.6 1.7m Total length of members = 29.5m
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1.27m 7.6m TYPE-2(T2) Panel length, s = 1.015m 1.7m Pitch angle, =16.2 Total length of members = 21.6m
1.463m 5.85m TYPE-3(T3)
Panel length, s = 1.2m 1.7m Pitch angle, =13.71 Total length of members =24.52m
1.74m 6.97m TYPE-4(T4)
Panel length, s = 1.625m 1.7m Pitch angle, =10.01 Total length of members =34.82m
1.6m 9.6m
TYPE -5(T5)
Panel length, s = 1.39m Pitch angle, =11.80 1.7m Total length of members =30.92m
1.4m
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8.14m
Purlin design
For the purlin section, choose RT-84 as a preliminary one. Dimension and properties are : Dimension nominal size, H = 80mm and B = 40mm Self weight, W = 5.19Kg/m = 50.91 KN/m Properties A = 6.61cm2
Ix = 52.25cm4 , Iy = 17.56cm4
Sx =13.06cm3 , Sy = 8.78cm3
rx = 2.81cm , ry = 1.63cm A) Cross-section classification
For Fe 430 steel, Fy = 275Mpa and
= = 0.92
Internal flange, C = b -3t = 31mm
= = 10.33 26(= 23.92) ………class 1
Web with N.A at mid depth, d = 80-3*3 = 71mm
= = 23.67 72 (=66.24) …………class 4
The section does fall in the class 4 and thus the elastic section modulus is used without reduction for determining the design capacities.
B) Design capacities m0 = material safety factor =1.1
i) Elastic moment capacity
My, Rd = = = 2.195KN.m
Mx, Rd = = = 3.265KN.m
ii) Shear capacity: the design plastic shear resistance is given by
Vpl, Rd =
Where Av is shear area and for RHS it is given by
Av = = = 4.53cm2
Then Vpl, Rd = =65.39KN
C) Loading
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i) Dead load, GK1(purlin) = 50.91N/m ,GK2 (roofing) = 130*1.3 =169N/m Total load,GK = 219.91N/m
ii) Live load qK = 0.25*13 = 0.325KN/m QK = 1KN/m ……..located at the center
Case 1: total design load X-axis, Pdx = 1.1*(219.91*sin) +1.35*(325* sin) = 148.478 Point load, Pdx2 = 1.35*1* sin = 1.35*1* sin12.6 = 294N Y-axis, Pdy =1.1*(219.91*cos) +1.35*(325*cos+370) =1163.76N/m And point load, Pdy2 = 1.35*cos12.6 =1317.5N
y 1317.5N x 294N 1163.76N/m 148.478N/m
z z 2.5m 2.5m
Design bending moments and shear forces at the critical sections are:
My,sd =
= = 0.2997KN.m My,Rd (=2.195KN.m) …ok!
Mx,sd =
=1.732KN.m Mx, Rd = 3.265KN.m………ok!!
Vsd,max = = 2.11KN Vpl,Rd = 65.39KN …ok!
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Check for combined action of shear and moment
= = 0.0323 0.5 no moment reduction
Check for combined effect
1.0
= = 0.667 1.0 ……ok!!
Check for deflection According to table 5.1 of EBCS-3, 1995 allowable deflection for roofs generally is
Smax = = =12.5mm
And z = = = 10.0mm
The actual deflection obtained using unfactored load is
x =
= [(5/384)*(0.12*2.54) + (0.22*2.53) /48] * 1/ (210*106*17.56*10-8) =3.60mm Similar, the other components is y = [(5/384)*(0.902*2.54) + (0.976*2.53) /48] * 1/(210*106*52.25*10-8) = 7.44mm Hence, the overall deflection or vertical deflection
= = 8.26mm 10mm
Therefore, the section is safe from deflection.
Case 2: Total design load X-axis: Pdx = 0.9(219.91*sin12.6) = 43.175N/m Y-axis: Pdy = 0.9(219.91*cos12.6) +1.6*(1476) = -2168.45N/m
x y 43.175N/m -2168.45N/m z z
2.5m 2.5m The design moment and shear are
My,sd = =0.034KN.m My,Rd (=2.195KN.m)
Mx,sd = = 1.69KN.m Mx,Rd (=3.265KN.m)
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Vsd,max = = 2.71KN Vpl,Rd (=65.39KN)
Check for shear effect on bending
= = 0.041 0.5 …..Ok!!
Therefore no reduction in the design moments is required. Check for combined effect
< 1.0
=1.69/3.265 +0.034/2.195 =0.533 1.0 ……..ok!!
Check for deflection From the above computation, allowable deflections are: Max =12.5mm and 2 =10mm But the actual deflection (vertical) is given as: =y*cos -x*sin where =12.6 Where x = (5/384)*[(0.048*2.54)/ (210*106*17.56*10-8)] = 0.662mm y = (5/384)*[(1.261*2.54)/ (210*106*52.25*10-8)] = 5.845mm After all = 5.845*cos12.6 - 0.662*sin12.6 = 5.56mm 10mm Therefore our section is safe for deflection.
STRESS ANALYSIS OF TRUSS
A) As a sample analysis and design of truss 1 is given. To determine the self weight of the truss we choose RT-64 section as a preliminary section for the truss members. Properties and resistance capacities of the section are as follows:
i) Dimension and properties y Nominal sizes, 60mm by 40mm Wall thickness, t =3mm Self weight, W = 41.59N/m A = 5.41cm2 = 541mm2 x Ix =25.38cm4 Iy = 13.44cm4
Sx =8.46cm3 Sy =6.72cm3
Ry =2.17cm Rx =1.58cm ii) Section capacity in tension For section in axial tension, the design plastic resistance as per EBCS-3, 1995(4.4) is:
Npl,Rd=
Where A - cross sectional area and is equal to 541mm2
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Fy = yield stress of the material =275Mpa m1 = material safety factor =1.1 Npl,Rd =541*275/1.1 = 135.25KN
iii) Section capacity in compression Classification for Fe 430 steel
= = 0.92
Internal flange : C=b -3t = 40 -3*3 = 31mm
= =10.33 26 (= 23.92) …class 1
For web where whole section is subjected to compression:
= =18 39 (=35.88) …..Class 1
Then the design compression resistance of the cross section is
Ncomb,Rd =
Where m0 = material partial safety factor for class 1,2 or 3 cross section m0 =1.1 Ncomb,Rd = 541*275/1.1
Loading Dead load
Total length of the truss members = 29.50m -self weight of the truss ,GK1 =41.59N/m *29.50m =1.226KN -self weight of the ceiling ,GK2 = (7.60*2.5*0.008*)*8 KN =1.216KN Total load ,GK = 2.442KN Since we have 7 panel joints 1.226/7 = 0.175KN And 1.216/7 = 0.174KN
Similarly for the 5.85m span the weight of the truss and the ceiling can be sketched.
DESIGN OF TRUSS
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In order to get the maximum design actions, we take three different combinations:Case 1 - Dead load +Live load (concentrated)Case 2 - Dead load + Live load (distributed)Case 3 - Dead load + wind load
=0.713KN.m From the above three cases, case 1 is the critical case which gives maximum moment, Mmax = 0.822KN.m Determination of reaction of purlins
Case-1 DL + LL (concentrated) 0.98KN
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0.268KN/m
2.5m
R = 0.825KN, but the reaction on a given truss at panel points is equal to 2R, however at the heel is equal to R.
0.825m 1.65m 1.65m 1.65m 1.65m 1.7m 1.65m 0.825m
5.85m
0.825KN 1.65KN 1.65KN 1.65KN
1.65KN 1.7m 1.65KN 0.825KN
1.7m 5.69m
CHAPTER-TWO
DESIGN OF SLAB
Slabs are horizontal structural elements which transfer service loads to the frame elements and their design should follow procedures. We have slabs of the types: solid slabs and ribbed slabs Ribbed slabs are preferred when we have long spans and they have advantages of the following - Easy to make partion walls -It has a very good sound proof -It provides good architectural view for the ceilings
Geometry
hf ≥ (S/10,50mm)
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D bw
bw ≥ 70mm
C/C 1.0m
If center to center spacing is >1.0 the gap between the ribs should be designed as slabs And this center to center spacing should be minimized for the following reasons -to minimize the effect or impact of concentrated loads -to decrease the size of the filling HCB -to increase the bond between the HCB and the ribs considering the above guide lines and from def lection requirement we fix our dimensions
hf =60mm D=300mm C/C =400mm bw =80mm And we assumed HCB of size shown below ` 200mm
40mm
400mm
Design procedures Step-1 Depth determination
d ( )*
Where: fyk=characteristics tensile strength of steel Le=effective span e=accounts for the boundary condition and span ration for slabsOverall depth, D = d + l+ s + c
Step-2 Suitable dimension for the ribbed should be assumed considering deflection requirement and construction suitability.
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Step-3 Loading
To calculate the loads on the ribbed the following data are assumed
a) Unit weight - PVC tile ………….. 16kN/m3
- Terrazzo tile........ 23kN/m3
- HCB………………14KN/m3
- cement screed….. 20KN/m3
- RCC……………… 24KN/m3
b) Dimensions - Head room = 2.7m - Partition wall height = 2.7m - Plaster thickness = 1.5cm
Computation of loading:
Lay out of typical floor plan with its select strip
A 5 m B 3.8m C 5m D 5 m E
A D G J 5
B E H K 4
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F I L O’ C 3 3’
C’ F’ I’ L’ 2’
B’ E’ H’ K’ N’ 2
G’
A’ D’ J’ M’ 1
A’ B’ C’ D’ E’ F’
4m 5m 4 m 3.56m 5m
For the span – AB
Dead load 2mm of PVC = 0.002*0.4*16 = 0.0128 kN/m 4.8cm of cement screed = 0.048*0.4*20 = 0.384 kN/m RC slab (topping) = 0.06*0.4*24 + 0.08*0.2*24 = 0.96 kN/m HCB with ceiling plaster = 1 kN/m (assumed value) Partition wall = 0.2*1.15*2.7*14*0.4/25 = 0.1391 kN/m Plastering = 0.03*1.15*2.7*20*0.4/25 = 0.0298 kN/m Total dead load = 2.526 kN/m
Live load
Since our building residential type we took live load is 2 kN/m2 from EBCS-2, 1995 Live load = 0.4m*2KN/m2 = 0.8 kN/m
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For the span – BC
Dead load 2mm of PVC = 0.002*0.4*16 = 0.0128 kN/m 4.8cm of cement screed = 0.048*0.4*20 = 0.384 kN/m RC slab (topping) = 0.06*0.4*24 + 0.08*0.2*24 = 0.96 kN/m
HCB with ceiling plaster = 1 kN/m Partition wall = (4.1+1.31)*2.7*0.1*14*0.4/25 = 0.327 kN/m Plastering = (4.1+1.31)*2.7*0.1*20*0.4/25 = 0.0339 kN/m Total dead load (DL) = 2.832 kN/m
Live load Live load (LL) = 0.4*2 = 0.8 kN/m
Design load
Pd = 1.3*DL + 1.6*LL = 1.3*2.832 + 1.6*0.8 = 4.962 kN/m Since the ration of self weight the partitions to the total design load is less than 20% we don’t need to use Reynolds method to determine an equivalent loads.
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Modeling We model the ribs as continuous beams and the direction of ribs is chosen in the shorter direction but some ribs run in the longer direction in contrast to the above theory for construction simplicity. We consider three cases for the application of live loads to know the critical reactions for design and a typical rib is taken to show the behavior of alternate loading along the spans For span – ABC
Case-1 When the live load act on span –AB
1.28
3.6823.284
A B C Case-2 When the live load acts on span –BC
1.28
3.284 3.682
A B CCase-3 When the live load acts on the whole span (fig)
1.28
3.284 3.682
A B C
The analysis of the ribs for the above load cases is done using SAP (v, 7.4) and a typical is taken to show shear and bending diagrams and for the other cases it is tabulated in the following table
Bending shear force diagram for rib ABC in there Cases
Case-1
14.49 6.59
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-9.26 11.81
-13.07
8.31 5.36
5m 5m
Case-2 11.29 9.79
-6.06 -15.01
-13.07
4.87 8.97
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Design for flexure
Material specification C-25 C1 = 0.086 S-300 C2 = 3003.23 Class- work m = 28.78 = 0.0187
For rib ABC
Design for flexure
Mspan = 8.97 KN.m
1-Check for the assumed depth for flexure
d > (M/(k*b))
K = 3.8126 (constant from material property) After substituting for moment in the above equation we get d = 171.49 < 232.0 i.e. safe for the flexure
2- Check for the section either rectangular or T-section
Effective width=min
Effective width, be = min
= 400mm Neutral axis N.A = 0.8*X X = m**d =0.5*(0.086-(0.0862 – 4*8.97*106/ (3000.23*400*2322))) =0.00162Then x=*m*d =0.00162*28.78*232 =10.98And y=0.8*x=0.8*10.98=8.79<60mm (there fore the section is rectangular of width be=400mm
3-reinforcement design
As= *be*d =0.00162*400*232 =150.48mm2
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#of bars 10 =150.48/78.54=1.92Use 2 10
M support =15.05KN.m
Similarly:
1) Check for flexure
d where M=15.05 KN.m
Substituting the value we get d=222.14<232mm (section is safe for flexure)
2) Check the section for its classification
The section is obviously rectangular r =0.5*(0.086-(0.0862 – 4*15.05*106/ (3000.23*80*2322))) =0.00165 3) Reinforcement design
As = *b*d 0.0165*80*232 =306.24
#of bars 14 = =1.988
Use 2 14A similar calculation can be applied for the other ribs and tabulated as shown below
Table 2.3 Design summary for ribs
Shear design
Let’s take rib ABC to show the procedure of design for shear From the there loading cases case- 3 (when the
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Ribs design moments reinforcement
span support span support
ABC 8.97 -15.05 2Ø10 2Ø14
DEF 14.11 -6.63 2Ø14 2Ø10
GHI 13.67 -6.63 2Ø14 2Ø10
JKL 13.4 -7.1 2Ø14 2Ø10
A'B'C' 11.65 -6.63 2Ø14 2Ø10
D'E'F' 14.84 -6.63 2Ø14 2Ø10
G'H'I' 5.06 -6.6 2Ø10 2Ø10
J'K'L' 15.17 -6.6 2Ø14 2Ø10
M'N'O' 9.26 -15.29 2Ø10 2Ø14
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A DESIGN OF (G+4) LOW COST BUILDING AND ITS COST ESTIMATION (BY USING RIBBED SLAB)
whole span is loaded with the live load) is critical for shear design (fig above)
The shear is max at
d= = .457m
Shear capacity
Concrete shear capacity
Vc = 0.25*k1*k2*fctd*bw*d bw = rib width =80mmd=effective depth =232mmk1=1.6-d=1.6-0.232=1.368 (d in m)
k2=1+50*r = = 1.0833
Vc = 0.25*1.368*1.083*1.031*80*232=7.087KN
Diagonal shear capacity
Vrd =0.25*fcd*bw*d =0.25*11.33*80*232 =52.57KNBut from theoretical point of view the shear capacity for T-section is 1.1 times than that of the rectangular section For span AB
Vdl= (3.11-.457)*15.41/3.11=13.14 KNVdl = (1.89-0.457)*9.39/1.89=7.12 KNTaking the maximum design shear force:For cases where Vc <Vd (reinforcement is needed)That means for Vd =13.14 KN Vs=Vd-Vc = (13.04-7.096) = 6.044 KN S =Asv*fyd*(d-dc)/Vs
=2*28.26*260.87*(232-43)/6.044 =461.1mm
But the maximum spacing, s max =min (d, 800, Asv *fyk/ (.4*bw)) mm =min (232,800,525) mm =232mm
Take 6 c/c 230mm
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Similarly for the other ribs the required shear reinforcements are minimum
Load transfer to beam from ribs
On block-1 On axis-3 31.04
Loading Weight of wall on beam = 0.2 * 2.7 *14 = 7.6 kN/m Reaction from ribs = 9.39 / 0.4 = 23.48 kN/m w = 31.08 kN/m On axis-4 83.88
63.88 61.14 64.03
A B C D E
Loading On AB Weight of wall = 7.6 kN/m Reaction from ribs = 75.85 kN/m w = 83.41 kN/mOn BC Weight of wall = 7.6 kN/m Reaction from ribs = 56.32 kN/m w = 63.88 kN/mOn CD Weight of wall = 7.6 kN/m Reaction from ribs = 53.57 kN/m w = 61.14 kN/mOn DE Weight of wall = 7.6 kN/m Reaction from ribs = 56.47 kN/m w = 64.03 kN/m
On axis-5 39.86 37.14 36.985
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30.71
A B C D E
Loading On AB Weight of wall = 7.6 kN/m Reaction from ribs = 23.15 kN/m w = 30.71 kN/m On BC Weight of wall = 7.6 kN/m Reaction from ribs = 32.3 kN/m w = 39.86 kN/m On CD Weight of wall = 7.6 kN/m Reaction from ribs = 29.58 kN/m w = 37.14 kN/m On DE Weight of wall = 7.6 kN/m Reaction from ribs = 29.425 kN/m w = 36.985 kN/m
On Block-2
On Axis-3’
30.36
Loading Weight of wall = 7.6 kN/m Reaction from ribs = 22.8 kN/m w = 30.36 kN/m On Axis-2
84.11 65.435 64.8451.91 58.46
A’ B’ C’ D’ E’ F’ Loading
On A’B’ Weight of wall = 7.6 kN/m Reaction from ribs = 76.55 kN/m w = 84.11 kN/m On B’C’ Weight of wall = 7.6 kN/m Reaction from ribs = 57.87 kN/m w = 65.435 kN/m
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On C’D’ Weight of wall = 7.6 kN/m Reaction from ribs = 44.35 kN/m w = 51.91 kN/m On D’E’ Weight of wall = 7.6 kN/m Reaction from ribs = 57.275 kN/m w = 64.835 kN/mOn E’F’ Weight of wall = 7.6 kN/m Reaction from ribs = 50.90 kN/m w = 58.46 kN/m
On axis 1-1
33.47 40.26 38.71 33.26
24.735 A’ B’ C’ D’ E’ F’
Loading On A’B’ Weight of wall = 7.6 kN/m Reaction from ribs = 25.15 kN/m w = 33.466 On B’C’ Weight of wall = 7.6 kN/m Reaction from ribs = 32.70 kN/m w = 40.26 kN/mOn C’D’ Weight of wall = 7.6 kN/m Reaction from ribs = 17.175 kN/m w = 24.735 kN/mOn D’E’ Weight of wall = 7.6 kN/m Reaction from ribs = 31.15 kN/m w = 38.710 kN/m On E’F’ Weight of wall = 7.6 kN/m Reaction from ribs = 25.70 kN/m w = 33.26 kN/m
Mass center and stiffness center calculation Table 2.4 Typical Floor 1 Mass Center Calculation (sample)
Items W(KN) Xi(m) Yi(m) Wxi(KN- Wyi(KN-m)
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A DESIGN OF (G+4) LOW COST BUILDING AND ITS COST ESTIMATION (BY USING RIBBED SLAB)
CHAPTER THREE
LATERAL LOAD ANALYSIS
The lateral loads to be considered for the design of a building are:- 1. Earth quake load and 2. Wind load NOTE: The analysis for both will be done and the critical load condition will be considered for the Design .
Earth Quake Analysis
According to EBCS-8,1995 static method of analysis is used. The seismic base shear force Fb for each main direction is determined by the equation : Fb=Sd*(T1)*W Where:- Sd*(T1)= Ordinate of the design spectrum T1=fundamental period of vibration of the structure for translational in direction Considered. W= seismic dead load computed. For linear analysis , the design spectrum Sd*(T1) normalized by the acceleration of gravity g is defined by the following expression :- Sd*(T) = ( EBCS-8,1995 Art 1.4.2.2 (4)) Where:- = The ratio of the design bed rock acceleration to the acceleration of gravity g and is given by:- =o*I
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o = bed rock acceleration ratio for the site and depend on the Seismic zone (Table 1.1) I = The importance factor (Table 2.4) For zone 4 building location (Mekelle) :- o = 0.1 and use I = 1.0 = 0.1*1.0 =0.1 = The design response factor for the site and is given by :- =1.2*S/(T)2/3 2.5 S= site coefficient for the soil characteristics. =1.0 (for For building up to 80m height the value of T1 may be approximated by the formula:- T1 = C1 *H2/3 (sec) Where :- H = Height of the building (m) = 18.7m C1= 0.075 for reinforced concrete moment resisting frames.
T1 = 0.075 (18.7)3/4 = 0.674 = 1.2*1/(0.62)2/3 The behavior factor to account for energy dissipation capacity is given by :- = o * KD*KR*KW 0.7 (EBCS-8,1995, art.3.3.2.1(1))
Where: o -basic value of the behavior factor , dependent on the structural . type (table 3.2) For frame system, o = 0.2 KD-factor reflecting the ductility class Use KD = 1.0 for DC’H’ KR-factor reflecting the structural regularity in elevation, for regular structures KR= 1.0 Kw-factor reflecting the prevailing failure mode in structural system with walls Kw= 1.0 for frame and frame equivalent dual systems
Fb= 0.03*8935.29 kN = 286.1 kN The concentrated force Ft at the top, which is in addition to Fn shall be determined from the equation: Ft = 0.07*T1* Fb (EBCS-8, 1995 art.2.3.3.2.3 (2))
= 0.07*0.62*286.1 = 12.42 kN The remaining portion of the base shear shall be distributed over the height of the structure, including level n according to:-
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Wind load analysis (for block-2)
External pressure
For the majority of the structures the resonant components are small and the wind load can be simplified by considering the background component only. The wind pressure acting on the external surface of structure we shall be obtained from. We = qref *ce(ze)*cpe…….. (EBCS-1, 1995 art.3.5.2 (1)) Where : qref = the reference wind pressure = 242 pa (previous result) Ce(ze) = exposure coefficient Exposure coefficient, ce (ze) , according to 3.8.5 (5) is given by :-
Ce(ze) = cr 2 (z)*ct
2(z)*
From table 3.2, for terrain category IV =0.24 , Zo = 1m and Zmin = 16mFor our case height of the building = 16.7m, hence cr
(z) = cr (Zmin)
= *ln ( )
Substituting the value: cr
(z) = 0.676 cr
(z) = 1.59Cpe = external pressure coefficient (according to ERBCS-1, 1995, table A.1) For A> 10m2
Cpe = Cpe,10
o Wind load in the shorter direction
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h =16.7m
e = min =min Use e= 22.92m
For case d < e:-
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h = 16.7m < b = 22.92m … the building is consider as one part qref = 242 N/m2 For zone D : We = 242*1.59*0.8 = 0.308 kN/m2
For zone E : We = 242*1.59*-0.3 = -0.115 k N/m2
Total external pressure on the building will be We = 0.308 + 0.115 = 0.423 k N/m2a
o Wind load in the longer direction
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zone Cpe valueD +0.8E -0.3A* -1.0B* -0.8
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A DESIGN OF (G+4) LOW COST BUILDING AND ITS COST ESTIMATION (BY USING RIBBED SLAB)
e = min =min use e = 10.30m
For the case d > e
h = 16.7m > b = 10.30m < 2*b = 20.6 Hence, the building is considered as two part, comprising: a lower part extending upwards from ground by a height equal to b and an upper with height to h.
cr (z = b = 10.30 < Zmin = 16 ) = 0.24*ln (16/1) = 0.665
cr (z = 16.7 ) = 0.676
ce (z = 10.30) = 0.665 2 *12* = 1.56
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ce (z = 16.7) = 0.6762 *12* = 1.59
, hence, we use linear interpolation for Cpe coefficient.
For zone D : We = 0.775*1.59*242 = 0.298 kN/m2, at Ze = 16.7m For zone E : We = -0.3*1.59*242 = -0.115 kN/m2, at Ze = 16.7m At Ze = b = 10.30m For zone D : We = 0.775*1.56*242 = 0.293 kN/m2
For zone E : We = -0.3*1.56*242 = -0.113 kN/m2
The total external pressure on the building will be : At Ze = b = 10.30m We = 0.293 +0.113 = 0.406 kN/m2
At Ze = h = 16.7 We = 0.293\8 + 0.115 = 0.413 kN/m2
Internal pressure
The wind pressure acting on the internal surface of structure Wi shall be obtained from: Wi = qref *Ce(Zi) * Cpi Where: Cpi – internal pressure coefficientFor closed building with internal partition and opening windows the extreme values are : Cpi = 0.8 or Cpi = -0.5…… EBCS-1, 1995, art.A.2.9 (16) Ce(Zi) = Ce(Ze) = 1.59 Wi = 242*1.59*0.8 = 0.3087 kN/m2
Wi = 242*1.59*-0.5 = -0.198 kN/m2
The net wind pressure will be : In the longer direction Wnet = 0.406 + 0.308 – (-0.192) = 0.906 kN/m2 at Ze = b = 10.30m Wnet = 0.413 + 0.308 – (-0.192) = 0.913 kN/m2 at Ze = h = 16.7m
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zone Cpe valueA -1.0B -0.8C -0.5D 0.775E -0.8
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A DESIGN OF (G+4) LOW COST BUILDING AND ITS COST ESTIMATION (BY USING RIBBED SLAB)
In the shorter direction Wnet = 0.423 + 0.308 – (-0.192) = 0.923 kN/m
Table for values of lateral loadsTable3.1comparison of wind force and earth forcefloor Wind load shorter direction
From the above result earth quake load is the critical which govern our design Note: - for block-1 we got the same result which is the critical one is the earth quake load.
Distribution of storey shear D-value method
The rigidity center for each floor is determined by:- Xs = (Dyi)*Xi/(Dyi) Ys = (Dxi)*Yi/(Dxi) Where:-Dx and Dy are shear distribution coefficient or D-value for X and Y direction respectively. Moment of inertia for beam and column: For beams
30X40 I = = 90*103 cm4
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30X30 I = = 67.5*103 cm4
45X45 I = = 341.72*103 cm4
For column
40X40 I = = 213.33*103 cm4
45X45 I = = 341.72*103 cm4
Stiffness ratio:- Stiffness ratio for a member is given by:
K = , where I = moment of inertia and L = length of a member
Calculation of D-values:
D = a* Kc
Where: a = and = for general case
a= and = for fixed base
Kb and Kc are stiffness ratio for beam and column express in terms of standard K K = 103cmThe stiffness ratio for each beam and column are as shown below for the selected frames
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A DESIGN OF (G+4) LOW COST BUILDING AND ITS COST ESTIMATION (BY USING RIBBED SLAB)
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A DESIGN OF (G+4) LOW COST BUILDING AND ITS COST ESTIMATION (BY USING RIBBED SLAB)
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A DESIGN OF (G+4) LOW COST BUILDING AND ITS COST ESTIMATION (BY USING RIBBED SLAB)
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D-value calculation for frame on axis-5
0.4 0.24 0.18 0.43 0.43 0.43
1.14 1.71 1.07
0.4 0.56 0.43
= = 0.62 = 0.502 = 0.402
= 0.414 a = 0.24 a = 0.4 a = 0.38
a = D = 0.15 D = 0.201 D = 0.153
= 0.172D = a* = 0.0713
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The center of rigidity is calculated as
Xs =
Ys =
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The center rigidity is calculated as
Xs =
Ys = , this values are the same for
floor two and three.
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the center of rigidity is calculated as
Xs =
Ys =
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The center of rigidity is calculated as
Xs =
Ys =
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The center of rigidity is calculated as
Xs =
Ys =
To allows for accidental torsional eccentricity location of mass center may be in error to either side by : eLi = 0.05 * Li
Where: Li = dimension of building plan perpendicular to the direction of earth quake loading
-when the earth quake is in the y-direction eLi = 0.05 * 18.8 = 0.94m
-when the earth quake is in the x-direction eLi = 0.05 * 10 = 0.5m
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Correction factor to account for torsional effect is given by:
Where : , -eccentricities from the center of rigidity for the two extreme positions of the storey shear.
Jx = Dy * X2 and Jy = Dx * Y2
Table3.2 The center of rigidity can be tabulated as follow for block 1
Floor Xc(m) Yc(m)Roof 7.430 6.710
Fourth 7.430 6.710Third 7.430 6.710
second 7.430 6.710First 7.430 6.710
Ground 7.580 6.670 Similarly; Table3.3 the center of rigidity can be tabulated as follow for building 2
Eccentricity calculation for building 1
exi = (Yc-Ym) eli (X-direction) eyi = (Xc-Xm) eli (Y-direction)
The calculated results are tabulated as follow for building Table3.4
Floor ey1 ey2 ex1 ex2
MEKELLE UNIVERSITY, FACULITY OF SCIENCE AND TECHNOLOGY DEPARMENT OF CIVIL ENG’G
Floor Xc(m) Yc(m)Roof 12.360 3.440
Fourth 12.170 3.500Third 12.170 3.500
second 12.170 3.500First 12.170 3.500
Ground 12.400 3.540
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A DESIGN OF (G+4) LOW COST BUILDING AND ITS COST ESTIMATION (BY USING RIBBED SLAB)
Ground -0.120 0.880-
1.180 0.700
Fourth 0.330 1.330-
4.840 -2.960
Third 0.330 1.330-
4.840 -2.960
second 0.330 1.330-
4.840 -2.960
First 0.330 1.330-
4.840 -2.960
Roof 0.350 1.350-
3.310 -1.430
Distribution of story shear in the X & Y direction for ground floor (sample) Base shear=286.1KN (for ground) Table3.5
Using the above result we will gett = 0.908 v = 0.419 Therefore, TRd, cor = 38.75 and VRd,cor = 18.3And the torsion and shear resistance of the concrete Tc,cor = tc *Tc Vc,cor = vc*Vc
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CHAPT –FIVE ER
Design of column Before designing columns the members should be classified as sway or non sway depending on their sensitivity to secondary effect.According to EBCS 2, 1995 Article 4.4.4.2:A frame may be classified as non sway if its response to in plane horizontal is sufficiently rigid for it to be acceptability accurate to neglect any additional reactions arising from horizontal displacement of its nodes. If a frame is classified as sway, the effect of the horizontal displacements of its nodes should be taken in to consideration in the design procedure. A frame may be classified as non sway for a given load case if the critical load ratio Nsd/Ncr 0.1Design procedure
1) To design a column in a particular frame first the frame should be classified as sway or non sway
2) To determine the nature of the selected frame we substitute the beams and columns by one substitute frame
3) The value of axial loads on each substitute frame is taken by adding the axial load of each column for the story including self weight (But the sap results already accounts such loads and they are directly taken for design
4) The value of the stiffness coefficients of the substitute fame is given by For beams = 2*kbi
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For columns =kci
Where Kbi = stiffness coefficient of beams Kci = stiffness coefficient of columns5) The effective length of the substitute frame is computed for each storey assuming
a sway frame as shown in the following equations For non sway
=
For sway mode Conservatively:
= (1+0.8 αm) 0.5
Where αm is a stiffness coefficient which can be discussed using the following theoretical model k1
k11 k12 α1= (k1+kc)/ α1 (k11+k12 kc
α1= (K2+kc)/ α1 (k21+k22) α1= (α1+ α2)/2 k21 k22
k2 Where k1 and k2 are column stiffness coefficients (=EI/L) K11, k12, k21, k22 are the boundary beam stiffness
Kc is the stiffness coefficient of the column being designed α =1.0 if opposite end elastically rigid α = 0.5 if opposite end free to rotate α = 0 for cantilever beam N.B The above approximate equations for effective length calculation are applicable for values of α1 and α2 not exceeding 10. If a base is designed to resist the column moment, α may be taken as 1.0
6) The dimension of the substitute column is computed to find the moment of inertia of the section, (Ic).
7) The amount of reinforcement required by the substitute column is computed, and the moment of inertia of the reinforcement with respect to the centroid of the concrete section is determined.
For more accurate determination, the first order moment, Mdl at the critical section of the substitute column may be determined using
Mdl = ( α 1+ 3)*H*L (α1+ α2+6) Where H =the total horizontal reaction at the bottom of the storey L=storey height
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8) The critical load of a storey may be assumed to be equal to that of the substitute beam-column frame and given as
Ncr = (Π2*EIe)/ (Le2)
Where EIe is the effective stiffness of the substitute column designed Le is effective length In lieu of more accurate determination, the effective stiffness of a column may be taken as EIe= 0.2*EcIc*+EsIs Where :- Ec =1100fcd Es is the modulus of elasticity of steel (in our case =2*10^5)
Ic & Is are the moment of inertia of the concrete and steel bars, respectively of the substitute column, with respect to the centroid of the concrete section We designed four columns but to show the procedure we select two columns How ever, before going to design let’s identify whether they are sway or non sway following the procedure as follows:
Frame on Axis D
0.065 0.13
0.8 0.8 1.51 0.14 0.28
0.8 0.8 1.51 0.14 0.28
0.8 0.14 0.8 1.51 0.28
0.8 1.51 0.14 0.8 0.28
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Level Nsd(KN V As(mm2 s(109) Ncr(KN Nsd/Ncr Classificationfoundation 1560.9 0.438 0.065 Min 3623 8 0.182 78862 0.02 Non sway ground 1459.6 0.41 0.081 Min 3623 8 0.182 13122 0.14 sway1st 1106.5 0.311 0.093 Min 3623 8 0.182 10687 0.131 sway2nd 753.67 0.212 0.075 Min 3623 8 0.182 10687 0.0895 Non sway 3rd 405.14 0.114 0.049 Min 3623 8 0.182 10687 0.0483 Non sway 4th 61.13 0.017 0.009 Min 3623 8 0.182 7398 0.0101 Non sway
Design of Selected Column For buildings a design method may be adopted which assumes that the compression members are isolated and have a simplified shape for the deformed axis of the column
Total eccentricity The total eccentricity to be used for design of column with constant cross section is given by: etot = ea+ee+e2
Where :-
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ee the equivalent constant first order eccentricity There are two cases to compute the equivalent eccentricity
1. for first order eccentricity eo equal at both ends of a column ee= eo
2. for first order moments varying linearly along the length, the equivalent eccentricity is the higher of the following two values
ee = 0.6eo2+0.4eo1
ee = 0.4eo2
eo2 & eo1 are first order eccentricity at the ends eo2 being positive and greater in magnitude than eo1. ea is the additional eccentricity to account for geometric imperfection introduced by increasing the eccentricity of the longitudinal force acting in the most un favorable condition.
ea = Le/300 ≥ 20mm , Le is the effective length of isolated column e2 is the second order eccentricity According to EBCS, 2, 1995 article 4.4.6(2) second order effects in compression members need not be taken in consideration in the following cases
a) for sway frames the greater of -25
- 15/Vd, and Vd =Nsd /fcd*Ac
b) for non sway frames 50-25(M1/M2) where :- M1& M2 are first order moments at the ends and M2 being always positive and greater in magnitude than M1,and M1 being positive if the member bent in a single curvature and negative if bent in bent in double curvature. For sway frames having ratio of Nsd/Ncr <0.25 second order effect is computed using the magnification factor, δs
δs = 1/ (1- Nsd/Ncr) Where :- Nsd =design value of the total axial load Ncr = the critical value for failure in sway mode And Mf = δs*M1 where :- Mf =the amplified sway moment M1= the first order moment at the point of total maximum moment.The total moment used for design of column at the critical section is given by: Mtot= Mf + Ma
As per our EBCS-2, 1995 As, max = 0.08*Ac As, min = 0.008*Ac
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4th 5.46 2.63 4.05 0.92 2.76 20 61.13 1.2226
For Second Order effectTable 5.7
Level Le Li Actual SR Critical SR 2nd order effect (Mtot) xfoundation 1.56 0.116 13.45 50 not considered 34.066Ground 4.95 0.116 42.67 50 not considered 34.1061st 5.28 0.116 45.52 50 not considered 30.9742nd 5.28 0.116 45.52 74.47 not considered 22.0583rd 5.28 0.116 45.52 71.16 not considered 16.484th 2.76 0.116 23.79 54.86 not considered 7.73
Level Le Li Actual SR Critical SR 2nd order effect (Mtot)y
foundation 1.556 0.116 13.41 48.03 not considered 83.83Ground 4.86 0.116 41.90 51.06 not considered 92.761st 5.28 0.116 45.52 68.636 not considered 41.92nd 2.649 0.116 22.84 61.37 not considered 33.813rd 2.649 0.116 22.84 51.786 not considered 32.424th 2.76 0.116 23.79 74.405 not considered 4.668
Table 5.12Final Design Summary Of column located at (axis 2, axis D)Level Nsd Mx My V x y s As providedfoundation 1560.9 34.07 83.83 0.874 0.05 0.12 0.31 2121.9 8Ground 1459.6 34.11 92.76 0.817 0.05 0.13 0.293 2005.5 1st 1106.5 30.97 41.9 1.08 0.101 0.137 0.66 2579.8 82nd 753.67 22.06 33.81 0.739 0.072 0.11 0.22 859.95 3rd 405.14 16.48 32.42 0.397 0.054 0.106 0.1 390.88 44th 61.13 7.73 4.668 0.088 0.044 0.002 min 500 4
Similar manner taken for a column of the other buildingTo design a column located at the intersection of frame 2’and frame B’ we follow the same procedure as above Frame On axis 2’Table 5.13Level m Le S L dlfoundation 1 1 1 2.683 626.03 1.28 163.37 2 163.37Ground 3.52 2.974 3.248 5.691 626.03 1.28 163.37 3 234.3271st 1.698 3.521 2.61 5.272 469.52 0.405 150.72 3 262.8162nd 1.698 1.698 1.698 4.607 469.52 0.405 121.53 3 182.2953rd 1.698 1.698 1.698 4.607 469.52 0.405 77.75 3 116.6254th 3.525 1.698 2.612 5.273 469.52 0.405 18.93 3 23.772
Table 5.14
level Nsd(KN) V As(mm2) s(109mm4) Ncr(KN) Nsd/Ncr Classification
foundation 1102.43 0.25 0.06 Min 3135 0.23 43807.32 0.025 Non sway
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Table 5.19 For second Order effectLevel Le Li Actual SR Critical SR 2nd order effect Mtot
foundation 1.56 0.087 17.93 70.83 Not considered 1 50.82Ground 3.75 0.087 43.10 25 considered 1.13 37.461st 3.81 0.087 43.79 25 considered 1.266 27.662nd 3.69 0.087 42.41 25 considered 1.24 18.853rd 2.13 0.087 24.48 57.16 Not considered 1 154th 2.16 0.072 30.00 63.7 Not considered 1 11.74
According to EBCS 2, 1995 article 7.2.4.3, (1) and (2)I. The diameter of should not be less than 6mmor one quarter of the diameter of the
diameter of the longitudinal bars II. The center to center spacing of lateral reinforcement shall not exceed:
-12 times the minimum diameter of longitudinal bars =12*16=192mm-Least dimension of column =400mm-300mm
According to EBCS 2, 1995 article 4.5.2. (1) in order to prevent diagonal compression failure in the concrete, the shear resistance Vrd of a section shall not be less than the applied shear force Vsd Where VRd = 0.25*fcd*bw*d bw =the minimum width of the web
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VR=0.25*11.33*400*300 =339.9KNTo compare the value for the maximum computed shear forces:Vsy =26.07 KN and Vsx = 33.09 KN taking the resultant force VR = 42.126 KNHence VRd=339.9 KN ≥ 42.126 KN....ok!For members subjected to axial compression the additional shear force VCRT carried by concrete is given by V CRT = 0.1* bw* d*Nsd/Ac …..EBCS-2, 1995 (4.30) Where:- Nsd is the design axial load For the minimum value of Nsd =69.50 KN V CRT = 0.1*400* 300*69.50/400*300 = 5.762 KN VRd= (339.9+5.762) KN and VR =42.126 KN since VR VRd apply min reinforcement. Ø 8 c/c 190mm
Basic anchorage length
The basic anchorage length is the embedment length required to develop the full design strength of a straight reinforcement bar The basic anchorage length, Lb for a bar of diameter Ø is given by Lb=Ø*fyd / (4*fbd)
The design bond strength for deformed bars is given by
Required anchorage length The required anchorage length Lb, net= (a* Lb *As, cal/ (As, provided)) ≥ Lb min
a=1 for straight bar anchorage in tension or compression Lb min= 0.6* Lb≥ 10Ø=200mm or Lb min=303.57mm≥200mm Lb, net=1.0*632.44*416.24/4398.22=598.79mm≥200mmUse Lb, net =590mm
Laps and jointsThe length of lap shall not be at least equal to Lo≥a1* lb net ≥ lo min....................EBCS2, 1995 (7.8) where Lo min = 0.3a*a1*Lb≥15Ø = 240mm for Ø16 = 300mm for Ø20 or 200mma1 a function of the percentage of the reinforcement lapped at any one section Assuming 100%lap, a1 =1.4 For Ø16, Lo min = 0.3*1.4*590* = 247.8mm
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Lo min = 240mm for Ø16 Lo min =300mm for Ø20 Lo≥ 1.4*590 = 826mm ≥ 300mm Use Lo = 830mm
CHAPTER-SIX
Foundation
Footing Design A) Interior column footing design (column at (4,E))
Y Using comb-4
MyGiven L - -Mx = 83.32 kN.m L’ Mx -My = -0.884 kN.m X -Pd = 1560.67 kN and L’ = B’ = 0.4 m B’
BAssuming an allowable bearing capacity for the soil as = 280 KPa
proportioning
Using unfactored load; Pd =
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1.3m
2m 0.7m
Assuming a surface footing, B = L
Solving the equation by trial and error, we get B = 2.19m We use B = L = 2.5m
Assume D = 0.70 and sub soil = 18 kN/m3 Dead weight of sub soil = (2.5*2.5-0.42)*1.3*18 = 142.51 kN Dead weight of footing = 2.5*2.5*0.7*25 = 109.38 kN Pd, tot = 1560.67 + (142.51 + 109.38 ) * 1.3 = 1888.1 kN
Taking maximum value from the above equation we get = 334.34 KPa
For conservative design Let’s check for both punching and wide beam shear failure respectively
i . punching shear
According to EBCS-2, 1995 article 4.7.6 the resistance of footing without punching shear reinforcement is give by: Vrd = 0.25 * fctd * k1 * k2 * u * d Where: K1 = 1+50 2.0
K2 = 1.6 – d 1.0 (d in meter)
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d =
e = Assume = 0.002, k1 = 1.0 + 50 * 0.002 = 1.1 L’+3*d L’ U = 4*(B’ + 3*d) = 4* ( 0.4 + 3*d) = 1.6 + 12*d Vrd = 0.25*1043*1.1*1.0*(1.6 + 12*d) B’ Vacting = (2.5*2.5 – (0.4 + 3* d)2)*334.34Then Vrd > Vacting (for safe condition) B’+3*d Hence solving for d d 499 mm
Therefore , D = 499 + 50 + 10 = 550 mm < 600 mm..... ok!.
ii - wide beam shear
According to EBCS-2, 1995, article 4.5.3, the shear force Vc carried by the concrete is given by : Vc = 0.2*fctd*k1*k2*bw*d Using 50mm clear cover and 20 longitudinal reinforcement bar d= 700 – 50 – 10 = 640 mm Vc = 0.25*1043*1.1*1*2.5*0.64 = 458.90 kN Vacting = (B/2 - B’/2 - d)*qu*B = (2.5/2 - 0.4/2 – 0.54) *333.27*2.5 = 342.69 kN Since Vc > Vacting ..... the section is safe !!
Similarly, By comb-1
Given F3 = 1928.028 kN and L’ = B’ = 0.4 m, = 280 KPa Mx = 5.435 kN.m My = 3.164 kN
proportioning
for unfactor , Pd =
Assume the square footing B = L
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Solving by trial and error we get B = 2.22 m Use B = L = 2.5 m then section is safe for both load combination
iii - reinforcement
M = 364.18*1*1.05*1.05/2 = 200.75 kN.mUsing table No.1 For design
= 22.14
Ks = 3.965 As = Ks * = 3.965 *
Amin = min * b*d = .002*1000*640 = 1280
Since As < Amin use Amin = 1280
taking 16
Take 16 c/c 150 mm (both direction)
N of reinforcement =
Hence provide 17 16 c/c 150 mm
iv-development length (check)
B) Exterior column footing design (column at (4,E))
Using comb-4 Given My Mx = 94.811 kN.m L L’ Mx My = -4.794 kN.m B’ P = 1067.78 kN and L’ = 0.4 m and B’ = 0.4 m B proportioning We assume an allowable bearing capacity for the soil as = 280 KPa
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Assume a surface footing B = L
Solving by trial and error we get B = 1.95 m, use B = 2.5
Assume D = 0.7 m Dead weight of sub soil = (2.5*2.5-0.*0.4)*1.3*18 = 142.05 kN Dead weight of footing = (2.5*2.5*0.7*25) = 109.4 kN Pd,tot = 1067.78 + 1.3*(109.4+142.04) = 1394.65 kN
= 261.40 kN
i - punching shear Vrd = 0.25*fctd*k1*k2*U*d U = 1.6 + 12*d Vrd = 0.25*1043*1.1*1*(1.6+12*d)*d Vacting = (2.5*2.5-(0.4+3*d)(0.4+3*d))*261.40 Vrd > Vacting for safe condition Solving by trial; and error d > 0.499m D = 499 + 50 + 10 = 600 mm < 700 mm ... ok! Hence D = 700 mm ii-wide beam shear
Verso = 0.25*fctd*k1*k2*bw*d, d = 700 – 50 – 10 = 0.640 mm = 0.25*1043*1.1*1*2.5*0.64 = 458.92 kN
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Let’s check the dimension for comb-1
Given P = 1258.36 kN B’ = 0.4 and L’ = 0.4 Mx = 7.65 kN.m = 280 KPa My = -2.62
Assume a square footing B = L
by trial and error B = 1.797 m < 2.5 m.... ok!
iii- reinforcement M = 261.4*1*1.05*1.05/2 = 144.96 kN
Km = 18.76 Ks = 3.95 (minimum) As = 894.675 mm2 < Asmin = 1280 mm2 1.05
Therefore take 16 c/c 150 mm (both direction)
N of bar 17 16 c/c 150 mm ult = 261.4 kN
iv - development length
y
C). footing at (axis-1 and axis-A’) Given P = 608.97 kN My Mx = 21.66 kN.m
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L L’ Mx
B’
B My = 19.98 kN.m and L’ = 0.35 and B’ = 0.25And we assume an allowable bearing capacity, = 280 KPa
B’= L’
proportioning using unfactored loads, Pd = 604.97/1.4 = 434.98 kN and ex = 0.0459 m and ey = 0.0497 m Assuming a square footing, B = L 1.4m
0.6m
After trial and error we get, B = 1.469 m take B = 1.5 m Assume D = 0.6 m and sub soil = 18 kN/m3
Dead weight of sub soil = (1.5*1.5 – 0.35*0.25)*1.4*18 = 54.495 kN Dead weight of footing = (1.5*1.5*0.6*25) = 33.75 kN Pd,tot = (608.97 + 1.3*(54.495 + 33.75)) = 723.68/8 kN ex = 0.0276 m ey = 0.0299 m ult = max = 395.62 KPa = max min = 261.49 Kpa
i - Check for punching
Vrd = 0.25*fctd*k1*k2*U*d = 1.4 + 12*d Vrd = 0.25*1043*1.1*1*(1.4 + 12*d) Vacting = (2*2 – (0.3 + 3*d0)*(0.4 + 3*d))*248.42 Hence solving for d , d 358.86mm L’
Then Vrd > Vacting ..... for safe condition 0.4+3*d Therefore D =358.86 + 50 + 10 = 418.86 mm B’ = 420 mm < 600 mm....ok !
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ii - Check for wide beam shear Vc = 0.25*1043*1.1*1.24*2.0*0.36 = 258.143 kN Vacting = (2/2 – 0.3/2 – 0.36)*248.42*20 = 243.45 kNSince Vacting < Vc ..............the section is safe!
iii - Reiforcement
M = 248.44*0.85*1.0*0.85/2 = 89.74 kN.m 0.4m 0.85m Km = 17.54 ks = minimum 0.3m As = 0.002*1000*540 = 1080 use 10 c/c 80 mm
D). Footing located at (axis-E and axis-3’) Given Mx =31.5 kN.m My = 16.07 kN.m 2.0m Pd =646.3 kN and L’ = 0.4 m and B’ = 0.3 m And we assume an allowable baring capacity for the soil as = 280.0KPa proportion
using un factor loads, pd = 0.035 m ex = 0.035m ey = 0.068 m Assuming a square footing, B = L
After trial and error, we get B = L = 1.52 m, and we use B = l = 2.0 m
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Assume, D = 0.6 m and sub soil = 18 kN/m3
Dead weight of sub soil = (2*2-0.4*0.3)*1.4*18 = 97.787 kN Dead weight of footing = 2*20.6*25 = 60 kN Pd,tot = 646.3 + 1.3*(60 + 97.78) = 851.41 kN ex = 0.0188 m ey = 00.369 m
I - Check for punching Vrd = 0.25*fctd*k18k2*U*d U = 2*(0.25+3*d) + 2*(0..35+3*d) = 1.2 + 12*d Vrd = 0.25*1043*1.1*1*(1.2 + 12*d) Vacting = (1.5*1.5-(0.35+3*d)(0.25+3*d))*395.62 Hence solving for d = 0.109 m , D = 169 mm < 600mm , d = 0.54m actually available depth ii - Wide beam shear
For roof inaccessible except for normal maintenance or other similar things, qk = 0.25 kN/m2
wind load qref = 242 Pa
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I-external pressure
Since the slab is at a height of h = 17.40 m Ce(z) = 1.62 For the external pressure coefficient, appendix A.2 of EBCS-1, 1995 is used. The roof is flat with a parapet of height
and
Because the roof is nearly square in shape, the coefficients are computed for one direction of the wind only.
1.22m e=min =4.87m
F2.44m 4.87m
G H I Table 7.1
1.22mF
0.487m 1.95m 2.29m Table 7.2 The coefficients are tabulated as followsZone F G H ICpe -2.08 -1.63 -0.711 -0.2 0.2Wind pressure -815.44 -639.03 -278.74 78.41 78.41 ii-internal pressure Wi = 313.63 Pa Wi = -196.02 Paiii-net wind pressure considering the severe condition Wnet = -815.44 – 313.63 = -1128.8 Pa = 78.41 – (-196.02) = 274.43 Pa
load combination the following three case are consideredcase-1: 1.3*DL + 1.6*LL Pd = 1.3*5.116 + 1.6*0.25 = 7.05 PaCase-2: 1.1*DL + 1.35*(LL + WL(+ve) ) Pd = 1.1*5.116+1.35*(0.25+0.274) = 6.34 Pa
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zone Area (m2)F 0.59G 1.19H 9.5I 11.15
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Case-3: 0.9*LL + 1.6*WL(-ve) Pd = 0.9*5.116 + 1.6*-1.128 = 2.799 paAmong the three case, case-1 is critical and used for analysis and designAnalysis Using table A-1 from EBCS-1, we take S9
a c xs=ys=0xf=0.056 Myf =Mxf = xf * Pd * Lx2
yf=0.056 = 0.056*7.05*4.722
S9 =8.83 kNm/m ux =uy = 0.33
Vxs = Vy = ux*Pd*Lx2
= 0.33*7.05*4.732
b d = 11.00 kN/mBut the load transferred to beam ab and ac
on ac w’ w’ = 0.989*11.00 = 10.879 kN/m self weight
reinforcement M = 8.83 kNm/m , d = 150 – 25 – 6 = 119 m Km = 24.97 , Ks = 3.99
As = but Asmin = min * b * d
= 0.002*1000*119 = 238 mm2 < As
Therefore s = use 8 c/c 160 mm
2-staircase design
We consider it to be simply support
C 1 2 D A…… ….. A
Rise = 200mmThread = 280mm
3 3
B……. …..B
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C C1 2
Modeling Axis 1-1
1.68m 1.37m 1.68m
Axis 2
1.68m 1.37m 1.68m
Axis 3-3
1.37m 2.13m 1.37m
Axis 3-3
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0.3m
0.167m
Depth determination
From deflection requirement for end span of a = 20
Using 16 bars and a cover of 15mm, overall depth becomes. D = 148.75 + 15 + 6 = 169.75mm Take D = 170mm, d = 149mmLoading
Data’s -Rise = 16.7 cm, thread = 30cm - # of rise = 6 and # of thread = 7 -terrazzo tile floor finishing of = 23kN/m3
Vdl = 37.56 From x = 0 to x =1.35 and x = 0 to x = -1.35 apply minimum reinforcement S = min = use 6 c/c 160mm From x = 0 to x = 1.35 and x = 1.35 to x = 1.978
In Foundation Columns. m3 11.00 13393.26 5.30 4,541.73
In grade beams m3 14.30 16327.87 25.19 19,941.66
In 10 cm thick ground floor slab m2 316.30 20008.51 411.31 32,561.36
Mild steel reinforcement according to structural drawings. Price includes cutting, bending, placing in position and tying wire
a) dia 6mm deformed bar Kg 2779.32 674.62 7,542.25
b) dia 8 mm deformed bar Kg 16081.79 2950.18 32,983.01
c) dia 12 mm deformed bar Kg 0 210.96 2,358.53
d) dia 14 mm deformed bar Kg 12980.23 6.41 71.66
e) dia 16 mm deformed bar Kg 14415.75 4823.99 53,932.21
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f) dia 20 mm deformed bar Kg 5880.25 595.74 6,660.37
g) dia 24 mm deformed bar Kg 29415 0.00
3.MASONARY WORK m3 86.10 29412 123.40 44,554.80 Subtotal 233711.79 337432.15
B-SUPER STRUCTURE 1. CONCRETE WORK
a) In elevation columns m3 57.20 76129.12 35.78 31,486.76
b) In suspended floor beams and top tie beam m3 95.60 108352.872 113.92 93,710.59
c) In roof slab . m3 3.27 3421 22.61 18,598.99
d) staircase m3 27.40 23136.85 24.70 20,318.22
e) beam column connections and necks of columns where indicated on the detail drawings. m3 10.08 11502.8
Floor slab m2 1361.60 102256.16 1188.30 94,362.90
precast beam 1 pcs 248 77475.2 0.00 0.00
precast beam2 pcs 112 34988.8 0.00 0.00
precast beam 3 0 0.00 0.00
precast beam 4 0 0.00 0.00
Slab blocketm2 58177.44
Mild steel reinforcement according to structural drawings. Price includes cutting, bending, placing in position and tying wire
a)dia 6 mm plain bar Kg 24309 3738.72 41,798.86 b) dia 8 mm deformed bar Kg 51064.97 5612.35 62,746.02 c) dia 10 mm deformed bar Kg 7612.92 661.06 7,390.63 d) dia 12 mm deformed bar Kg 30632.6 123.01 1,375.25 e) dia 14 mm deformed bar Kg 64897.75 2659.12 29,728.96 f) dia 16 mm deformed bar Kg 55566.75 1470.52 16,440.41 g) dia 20 mm deformed bar Kg 92364 1493.34 16,695.54 h) dia 24 mm deformed bar Kg 0 291.45 3,258.41Sub total 821888.232 Total 1055600.02 898250.17
Summary for comparison item Ribbed Pre cast DifferenceTotal Bars(kg) 25311.46 39529 14217.54
Total Volume(m3) 301.67 251.65 -50.02Total cost (birr) 898250.2 1055600 157349.852
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