Technical Note
19
slab and beams;
c - Reinforcement calculated and reported by the program for minimum
requirements of the code, strength check, initial condition, or other code related
criteria; and
d - Post-tensioning tendons defined by the user, each with its own location and
force.
4. The program matches the calculated moment (Ma) of each finite element cell with the
existing reinforcement in that cell. Using the parameters given below, the Program
calculates the effective moment of inertia for each cell:
a. Finite element cell thickness (to obtain uncracked second moment of area);
b. Available reinforcement associated with each cell (nonprestressed and
prestressed), with recognition of orientation and height of each individual
reinforcement;
c. Cracking moment of inertia associated with each cell in each direction (lcr);
d. Cracking moment associated with each cell (Mcr); and
e. Applied moment (Ma calculated in 2).
5. Having determined the effective second moment of area of each finite element cell in
each of the principal directions, the Program re-constructs the stiffness matrix of each
cell.
6. The Program re-assembles the system stiffness matrix and solves for deflections. At this
stage the solution given from the first iteration is a conservative estimate for the floor
deflection with cracking. For practical engineering design, it is recommended to stop the
computations at this stage.
For a more accurate solution the newly calculated deflection can be compared with that of a
previous iteration. If the change in maximum deflection is more than a pre-defined tolerance, the
Program will go into another iteration starting from step (2). In this scenario, the iterations are
continued, until the solution converges to within the pre-defined tolerance.
The Program accounts for loss of bending stiffness in beams and slab regions and its
combinations..
EXAMPLE
Using finite elements determine the deflection of the panel identified in Fig. EX1 for the loads
and conditions described in Example 1.
Calculate the deflection for the combination of dead and live loads.
Use ACI318-08 to determine the reinforcement necessary for both the in-service and strength
requirements of the code.
Use the calculated minimum reinforcement of the code to determine the cracked deflection. No
other reinforcement is added.
Using the above requirements, the cracked deflection of the floor system is calculated and
illustrated as a contour image in Fig. EX4-1. The deflection at the center of the panel under
consideration is 0.70 in. (17.78 mm) compared to 0.54 in. (13.72 mm) for the uncracked slab.
The cracked deflection can be reduced by adding reinforcement at the locations of crack
formation in addition to the minimum requirements of the code already included in the analysis.
Technical Note
20
FIGURE EX4-1 DEFLECTION CONTOUR OF SLAB WITH CRACKING
The locations of crack formation and the extent of cracking are illustrated in Figs. EX4-2 and
EX4-3. At each location, the reduction in effective moment of inertia is based on the calculated
moment at that location and the amount, position and orientation of reinforcement at the same
location. The largest loss of stiffness occurs over the columns and the support lines joining the
columns. The maximum loss of stiffness is 69% reducing the effective moment of inertia to 31%
of its uncracked value.
Technical Note
21
FIGURE EX4-2 EXTENT OF CRACKING SHOWN THROUGH REDUCTION IN EFFECTIVE
MOMENT OF INERTIA Ie ABOUT Y-Y AXIS
FIGURE EX4-3 EXTENT OF CRACKING SHOWN THROUGH REDUCTION IN EFFECTIVE
MOMENT OF INERTIA Ie ABOUT X-X AXIS
Technical Note
22
Deflection of Post-Tensioned Floor Systems
Two-way post-tensioned floor systems designed to ACI-318 provisions and the PTI-
recommended slab-to-depth ratios (Table 4), either do not crack under service condition, or
crack to an extent that does not invalidate calculations based on gross cross-sectional geometry
and linear elastic theory. This is because, unlike other major non-US codes, the allowable
tensile stresses in ACI are relatively low.
The preceding observation does not hold true for post-tensioned one-way slab and beams,
where ACI-318 permits designs based on post-cracking regime. For such post-tensioned floor
systems, designers must include allowance for cracking in their designs.
COMPARISON OF DEFLECTION CALCULATION METHODS
As illustrated in the design examples, the calculated deflections design engineers use from the ???
currently available procedures for conventionally reinforced concrete vary greatly. Table 6 lists the
outcome of the various methods. Note that for the typical floor system selected, the difference between
the various methods can be as much as three times. Finite Element Method with due allowance for
crack formation gives the largest deflection. The strip method with no allowance for cracking produces
the smallest value.
TABLE 6 DEFLECTION VALUES AT CENTER OF PANEL OF THE NUMERICAL
Calculation
Method
Deflection
in(mm)
Normalized Deflection
1
Closed form formulas
0.480(12.19)
69 %
2
ACI318 – Simplified method
0.528(13.42)
75 %
3
Strip method (uncracked)
0.462(11.74)
66 %
4
Strip method with cracking
and numerical integration
0.470(11.94) 67
%
5
Finite Element Method (FEM)
No allowance for cracking
0.540(13.72) 77
%
6
Finite Element Method (FEM)
With allowance for cracking
0.700(17.78) 100
%
Technical Note
23
LONG-TERM DEFLECTIONS
A concrete member’s deformation changes with time due to shrinkage and creep. Shrinkage of
concrete is due to loss of moisture. Creep is increase in displacement under stress. Under constant
loading, such as selfweight, the effect of creep diminishes with time. Likewise, under normal conditions,
with loss of moisture, the effect of deformation due to shrinkage diminishes. Restraint of supports to
free shortening of a slab due to shrinkage or creep can lead to cracking of slabs and thereby an
increase in deflection due to gravity loads.
While it is practical to determine the increase in instantaneous deflection of a floor system due to creep
and shrinkage at different time intervals, the common practice for residential and commercial buildings
is to estimate the long-term deflection due to ultimate effects of creep and shrinkage.
Shrinkage
It is the long-term shrinkage due to loss of moisture through the entire volume of concrete that
impacts a slab’s deformation. Plastic shrinkage that takes place within the first few hours of
placing of concrete does not play a significant role in slab’s deflection and its impact in long-
term deflection is not considered.
Long-term shrinkage results in shortening of a member. On its own, long-term shrinkage does
not result in vertical displacement of a floor system. It is the presence of non-symmetrical
reinforcement within the depth of a slab that curls it (warping) toward the face with less or no
reinforcement. The slab curling is affine to its deflection due to selfweight, and hence results in
a magnification of slab’s natural deflection.
It is important to note that, deflection due to shrinkage alone is independent of the natural
deflection of slab. It neither depends on the direction of deflection due to applied loads, nor the
magnitude. The shrinkage deflection depends primarily on the amount and position of
reinforcement in slab.
A corollary impact of shrinkage is crack formation due to restraint of the supports. This is further
discussed in connection with the restraint of supports. It is the crack formation due to shrinkage
that increases deflection under gravity loads.
Shrinkage takes place over a time period extending beyond a year. While the amount of
shrinkage and its impact on deflection can be calculated at shorter intervals, the common
practice is to estimate the long-term deflection due to the ultimate shrinkage value.
Shrinkage values can vary from zero, when concrete is fully immersed in water to 800 micro
strain. Typical ultimate shrinkage values are between 400 to 500 micro strain.
Creep
Creep is stress related. It is a continued magnification of the spontaneous displacement of a
member with reduced rate of creep with time. Values of creep vary from 1.5 to 4. Typical
ultimate creep values for commercial and building structures are between 2 to 3.
Restraint of Supports
Restraint of supports, such as walls and columns to free movement of a slab due to shrinkage
can lead to tensile stresses in the slab and early cracking under applied loads. Early cracking
will reduce the stiffness of the slab and increase its deflection.
Technical Note
24
Multiplier Factors for Long-Term Deflections
For design purposes, the long-term deflection of a floor system due to creep and shrinkage can
be expressed as a multiplier to its instantaneous deflection.
Long-term deflection due to sustained load:
Δ
l
= C *
Δ
i
(8)
Where
Δ
l
= long-term deflection;
Δ
i
= instantaneous deflection; and
C = multiplier.
ACI-318 suggests the multiplier factor shown in Fig. 5 to estimate long term deflections due to
sustained loads
FIGURE 5 MULTIPLIER FOR LONG-TERM DEFLECTION
The multiplier can be reduced, if compression reinforcement is present. The factor (
λ) for the
reduction of the multiplier is given by:
λ = C / (1 + 50
ρ’
)
(9)
Where
ρ’
is the value of percentage of compression rebar at mid-span for simple and
continuous members and at support for cantilevers.
ACI’s recommended multipliers account for the cracking of slab. Hence, they are intended to be
applied to cracked deflections. Several Investigators recommend long--term multiplier
coefficients for deflections based on gross cross-sectional area. These coefficients are higher
Technical Note
25
than the ACI-318 multiplier (Fig. 5). Table 7 lists the recommended values of multipliers for non-
prestressed slabs.
Δ
l
= ( 1 +
λ
c
+
λ
sh
) *
Δ
i
(10)
Where
λ
c
= creep multiplier;
λ
sh
= shrinkage multiplier;
Or, simply
Δ
l
= C *
Δ
I
, where C = ( 1 +
λ
c
+
λ
sh
)
TABLE 7 MULTIPLIERS FOR LONG-TERM DEFLECTIONS
Source
Immediate
deflection
Creep
λ
c
Shrinkage
λ
sh
Total
C
Sbarounis(1984) 1.0 2.8 1.2 5.0
Branson(1977) 1.0
2.0 1.0 4.0
Graham and
Scanlon (1986b)
1.0 2.0 2.0 5.0
ACI-318 1.0 2.0
3.0
Based on the author’s observation and experience, it is recommended that structures built in California
use the following values:
For conventionally reinforced floor systems
C = 4
For post-tensioned floor systems
C
= 3
LOAD COMBINATIONS
The load combination proposed for evaluating the deflection of a floor system depends on the objective
of the floors evaluation. The following describe several common scenarios.
Total Long-Term Displacement From Removal of Forms
(1.0*SW + 1.0*SDL + 1.0*PT + 0.3*LL)* C
Where
SW = selfweight;
SDL = superimposed dead load, (floor cover and partitions);
PT
= post-tensioning; and
LL
= design live load.
The above load combination is conservative as it assumes the application of superimposed
loads as well as the application of sustained live load of the structure to take place at the time
of removal of the supports below the cast floort. The factor 0.3 suggested for live load is for
Technical Note
26
“sustained” load combination. The significance of the above load combination is that it provides
a measure for the total deflection from the position of the forms at the time of concrete casting.
Its magnitude must be evaluated for aesthetics and drainage of surface water, if applicable. It is
used for checking the deflection of parking structure decks or roofs, where the floor is placed in
service in its as-cast condition.
Load Combination for Code Checks
For the acceptability of a floor deflection in connection with the code specified maximum values
listed in Table 1, the following two load combinations apply.
1.0*LL
C1*C*(SW + SDL + PT) + 0.3*C2*C*LL + 0.7*LL
Where C1 is the fraction of long-term deflection coefficient related to the balance of long-term
deflection subsequent to construction installation likely to be damaged by deflection of slab.
Partitions and other fixtures are generally installed when more than one-half of long-term
deflection has taken place. As a result, C1 is generally less than 50% of the long-term deflection
multiplier, assuming that the superimposed dead load and partitions are not installed before 40
days from date of casting the floor (Fig. 6). C2 relates to the time, when construction is complete
and in-service live load applied. This is generally less than 20% of the long-term multiplier.
Figure 6 can be used as a guideline for values of C1 and C2. For example, if the in-service live
load of a structure is put in place six months subsequent to casting the floor, the value of C2 will
be approximately 0.25 (value associated with 180 days in Fig. 6).
FIGURE 6 LONG-TERM SHORTENING OF CONCRETE MEMBERS DUE TO
CREEP AND SHRINKAGE WITH TIME
LIVE LOAD DEFLECTION
Technical Note
27
Even when using linear elastic theory to calculate a floor system’s deflection, cracking will result in a
non-linear response. For the same load, the deflection of a slab depends on the extent of cracking prior
to the application of the load. Therefore, when calculating the deflection due to the instantaneous
application of live load, one must use the following procedure:
Deflection due to LL = (deflection due to DL+LL) – (deflection due to DL)
The above accounts for loss of stiffness due to dead load prior to the application of live load.
APPENDIX A
CHARACTERISTICS OF PARISSA APARTMENTS TYPICAL FLOOR
Geometry
Slab thickness and support dimensions (see plan)
Concrete
f’c (28 day cylinder strength)
= 5000 psi (34.47 MPa)
Wc (unit weight)
= 150 pcf (2403 kg/m
3
)
Ec (modulus of elasticity at 28 days)
= 4,287 ksi (29558 MPa)
Non-Prestressed Reinforcement
Yield stress
= 60 ksi (400 MPa)
REFERENCES
Aalami, B. O. and Bommer, A. (1999) “Design Fundamentals of Post-Tensioned Concrete Floors,”
Post-Tensioning Institute, Phoenix, AZ, pp. 184.
ACI318-08
Bares, R., (1971), “Tables for the Analysis of Plates, Slabs and Diaphragms Based on the Elastic
Theory,” Bauverlag GmbH, Wiesbaden und Berlin, 1971, pp. 626
Branson, D. E., (1977), “
Deformation of Concrete Structures
,” McGraw-Hill Book Company, New York,
pp. 546.
Graham, C. J., and Scanlon, A., (1986), “
Long Time Multipliers for Estimating Two-Way Slab
Deflections
,” ACI Journal, Proceedings V. 83, No.5, pp. 899-908.
PTI (1990). Post-Tensioning Manual, 5
th
Edition, Post-Tensioning Institute, Phoenix, AZ, pp. 406
Technical Note
28
Sarbounis, J. A., (1994) “
Multistory Flat Plate Buildings: Measured and Computed One-Year
Deflections,
” Concrete International, Vol. 6, No. 8, August, pp. 31-35.
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