- Article
- Open Access
Crack Opening Behavior of Concrete Reinforced with High Strength Reinforcing Steel
- Amir Soltani^{1}Email author,
- Kent A. Harries^{2} and
- Bahram M. Shahrooz^{3}
https://doi.org/10.1007/s40069-013-0054-z
© The Author(s) 2013
- Received: 29 January 2013
- Accepted: 16 August 2013
- Published: 6 December 2013
Abstract
A major difference between high-strength reinforcing steel and conventional steel in concrete is that the service-load steel stress is expected to be greater. Consequently, the service-load steel strains are greater affecting cracking behavior. A parametric study investigating crack widths and patterns in reinforced concrete prisms is presented in order to establish limits to the service-load steel stress and strain. Additionally, based on the results of available flexural tests, crack widths at service load levels were evaluated and found to be within presently accepted limits for highway bridge structures, and were predictable using current AASHTO provisions. A limitation on service-level stresses of f_{ s } ≤ 414 MPa (60 ksi) is nonetheless recommended.
Keywords
- crack opening
- crack width
- bond characteristics
- high-strength reinforcing steel
1 Introduction
Reinforced concrete members are typically designed based on strength at ultimate limit state and subsequently checked for deflection and crack control at serviceability limit state. Although the service checks are generally conservative—based on limiting stresses in the structure at service loads—the adoption of higher strength materials suggests potential problems under service conditions. The material strength of steel reinforcement and concrete, bond characteristics, size of a member, and amount of reinforcement are all factors affecting the development of cracks in reinforced concrete members. Concrete members reinforced with high strength steel reinforcement [having a yield strength, f_{ y }, greater than 690 MPa (100 ksi)] have different behavior due to the expected higher service loads, compared to concrete members reinforced with conventional steel bars [f_{ y } = 414 MPa (60 ksi)]. Using a higher strength reinforcing steel could provide various benefits to the concrete construction industry by reducing member cross sections and reinforcement quantities, which would lead to savings in materials, shipping, and placement costs. Reducing reinforcement quantities may also reduce congestion problems leading to better quality of construction. Finally, coupling high-strength steel reinforcement with high-performance concrete should result in a more efficient use of both materials. This approach, however, affects the flexural stiffness, as measured by the effective moment of inertia, I_{ e }, of a cracked reinforced concrete member and results in different deflection and cracking behaviors.
1.1 High Strength Reinforcing Steel
The design of reinforced concrete structures in the United States is dominated by the use of steel reinforcement with yield strength, f_{ y }, equal to 414 MPa (60 ksi). Design with steel having higher yield strength values is permitted although the yield strength used in strength calculations is limited. Currently, ACI 318 (2011) permits design using steel reinforcement with yield strength not exceeding 552 MPa (80 ksi). The AASHTO LRFD Bridge Design Specifications (AASHTO 2010) similarly limit the use of reinforcing steel yield strength in design to no less than 414 MPa (60 ksi) and no greater than 517 MPa (75 ksi), although exceptions are permitted with owner’s approval. Both ACI and AASHTO limits have been written and interpreted to not exclude the use of higher strength grades of steel, but only to limit the value of yield strength that may be used in design, thus, reducing the efficiency of using these materials.
The limits on yield strength are required to ensure adequate ductility of a section and are related to the prescribed limit on concrete compressive strain of 0.003. The limits on yield strength also serve to control of crack widths at service loads. Crack width is a function of steel strain and consequently steel stress (Nawy 1968). Therefore, the stress in the steel reinforcement will always need to be limited to some extent in order to prevent cracking from affecting serviceability of the structure. However, with recent improvements to the properties of concrete, the ACI 318 limit of 552 MPa (80 ksi) and AASHTO limit of 517 MPa (75 ksi) on the steel reinforcement yield strength are believed to be unnecessarily conservative for new designs. Additionally, an argument can be made that if a higher strength reinforcing steel is used but not fully taken into account in design, there may be an inherent overstrength in the member that has not been properly incorporated in design.
Steel reinforcement with yield strength exceeding 552 MPa (80 ksi) is commercially available and being used in the United States. ASTM A1035 (2009) is specified to exceed 690 MPa (100 ksi) or 827 MPa (120 ksi).
2 Crack Formation and Crack Control
Crack formation refers to the incidence of any narrow, irregular opening of indefinite dimensions resulting from shrinkage, flexural or direct tension stresses, or internal expansion resulting from the products of corrosion or deleterious aggregates. The incidence of flexural and direct tension cracking that occurs at various stages is defined in relation to the stresses in the reinforcement at the cracked section (Reis et al. 1964). Since steel has a constant Young’s modulus (at service load levels) regardless of grade, this approach is possibly better described with respect to steel strain, rather than stress. The following brief description of load-induced cracking in a tension zone is based on that reported by Reis et al.
The first stage of cracking is concerned with those cracks produced by shrinkage, corrosive effects, and low flexural loads in which the measured steel strain is well below ε_{ s } = 0.0005 [f_{ s } ≈ 100 MPa (14 ksi)]. Cracks of this type are referred to as primary cracks. The second stage of cracking is concerned with those cracks that result from the difference in inextensibility between the concrete and steel, and the bonding forces that exist between the two. Cracks formed by this mechanism are referred to as secondary cracks. Secondary crack formation is usually studied by examining the portion of the beam between two adjacent primary cracks or by analyzing the model of an axially loaded reinforced concrete prism in tension (as is done in this study). The steel strains during the second stage of cracking are usually greater than 0.0005. There is considerable disagreement among the theories of secondary cracking concerning the significance of the variables involved, especially the nature of the bond stress distribution along the reinforcement between adjacent primary cracks. The third stage of cracking, also referred to as the equilibrium stage, occurs when no further secondary cracks can be formed, and existing cracks continue to widen. The steel strain is usually greater than 0.001 [f_{ s } ≈ 200 MPa (30 ksi)] at this stage of cracking. Although the initiation of primary cracks is important, the main concern of this research is with the distribution of second and third stage cracks, which occur at higher steel stresses.
When a reinforced concrete member is loaded gradually in pure tension, cracking of the concrete will take place in one or more places along the length of the member when the tensile stress in the concrete exceeds the tensile strength of the concrete. After cracking, the tensile stress in the concrete adjacent to the crack is relieved because of the slip that takes place between the concrete and reinforcement at this location. Away from the crack, tensile stress in the concrete between cracks is present because of the bond between the reinforcement and concrete. The distribution and magnitude of the bond stress along the reinforcement will determine the distribution of the concrete stress between cracks along the length of the member. As tension loading is increased, cracking will continue to take place until the stress in the concrete between cracks no longer exceeds the concrete tensile strength. This stage occurs due to excessive slip and the reduction of distance between cracks. Essentially, the distance between cracks becomes sufficiently small that the stress to cause concrete cracking can no longer be developed by the reinforcing steel present. When this condition is reached, the crack spacing reaches its minimum, but the crack widths will continue to increase as the tensile stress in the reinforcement increases (i.e., third stage cracking as described by Reis et al. 1964). Assuming this behavior to be valid and that second stage cracking is fully developed by ε_{ s } = 0.001 (Reis et al. 1964), it may be hypothesized that crack patterns in members having high strength reinforcing steel will not vary from those having conventional steel. Thus, only crack width, and not crack spacing, will be affected by utilizing the higher strength steel. The cracking behavior of reinforced concrete members in axial tension is similar to that of flexural members, except that the maximum crack width is larger than that predicted by the expressions for flexural members (Broms 1965a, b). The lack of strain gradient and restraint imposed by the compression zone of flexural members is probably the reason for the lower flexural crack width.
The final crack pattern in a member is determined at the end of the second stage of cracking (Reis et al. 1964). Therefore, controlling the spacing and width of secondary cracks are most important to the overall performance of a member. Based on the early studies reported above, the following are the main factors involved in the control of the final crack pattern: (a) reinforcement stress, (b) the bond characteristics of reinforcement, (c) the distribution of reinforcement over the effective concrete area subject to tension, (d) the diameter of reinforcement, (e) the percentage of reinforcement, (f) the concrete cover over the reinforcement, and (g) the material properties of the concrete.
Since the recalibration of ACI 318 load factors in 2002, Eq. 2 is calibrated for a de facto assumed crack width of w_{ c } = 0.46 mm (0.018 in.).
For Class 1 exposure (moderate exposure), the equation is calibrated, through γ_{ d } = 1, for a crack width of 0.43 mm (0.017 in.); for Class 2 exposure (severe exposure), γ_{ d } = 0.75. The de facto crack width (γ_{ d }) is 0.43 mm.
In members having high-strength reinforcing bars, early studies showed that an increase in crack width is due to an increase in steel stress and, to a lesser extent, due to an increase in the curvature of the member. Thomas (1936) pointed out that an increase in the curvature at a constant steel stress tends to distribute the cracking rather than widening individual cracks. An increase in the steel stress affects the difference in the elongation between the reinforcing steel and concrete and causes additional slip to occur. This slip is the main cause of the increase in crack size. Slip occurs in the vicinity of a crack and extends to a point where the differential strain is zero. At that point the bond stress and resistance to slip reach maximum values and decrease toward the mid-point between cracks. The overall values of bond force decrease with an increase in load. This decrease is attributed to (a) the effects of the increase in transverse contraction of the reinforcing bar (i.e., Poisson effect) and (b) the deterioration of the concrete at the concrete-steel interface (Odman 1962). Therefore, the crack width increases while the crack spacing remains constant. If the load is increased further, the slip between concrete and reinforcement continues to increase. Due to the comparatively low values of concrete extensibility, the increase in crack width can be considered essentially equal to the accumulation of the slip between adjacent cracks.
3 Research Significance
The adopted equations for calculation of crack width and crack spacing are based on the use of conventional steel. However, concrete members reinforced with high strength steel reinforcement [having a yield strength, f_{ y }, greater than 690 MPa (100 ksi)] have different behavior due to the expected higher service loads. An empirical parametric procedure has been introduced for determination of crack opening (crack width and crack spacing) in a reinforced concrete prism. Effective parameters have been investigated and finally the result has been compared to the available experimental data.
4 Parametric Study of Crack Characterization
In the case of using conventional steel bars in flexural members, it has been shown that during the second stage of cracking, when steel strains are usually greater than 0.0005, the presence of existing primary cracks affects the formation of secondary cracks under increasing moment. Away from a primary crack, stresses are transferred by bond from the reinforcement to the concrete. If enough force is transferred from the steel at the crack to the concrete away from the crack, the strains that are developed may exceed the strain capacity or the tensile strength of the concrete at a section and another crack will form perpendicular to the reinforcement. Theoretically, the section at which secondary crack formation occurs is midway between existing cracks. This mechanism continues until the tensile forces developed through bond transfer are insufficient to produce additional cracks. To compare and demonstrate the crack behavior of members reinforced with conventional steel bars and members reinforced with high-strength steel bars, a relatively complex material modeling in a simple direct tension model is used.
If L_{1} is sufficiently long to transfer a cumulative tensile stress resulting in a concrete stress, f_{ c }, greater than ultimate tension capacity of concrete f_{ cr }, then cracks will form. At the same stress level, additional cracks will continue to develop until the distance between adjacent cracks is no longer adequate to transfer sufficient tension to develop a new crack.
While the tension load (T) increases beyond that causing the first series of cracks, the relative strain in the reinforcement at the loaded ends and cracks will increase. According to Fig. 3, the arbitrary location where strain in the reinforcement is equal to the strain in the concrete (Point B) occurs at a distance L_{ 2 } > L_{ 1 }. In this case, the bond stress distribution along the length of the reinforcement corresponding to the tension force will be in a new form in which the angle of the descending branch, α, decreases (in Fig. 3, α_{ 2 } < α_{ 1 }). The cumulative bond stress increases while α decreases. As a result, more force is transferred to the concrete section; and the additional force may or may not cause more cracks between the first cracks. The process continues until the transferred tension stress in the concrete section no longer exceeds f_{ cr }.
4.1 Crack Behavior for a Concrete Prism Reinforced with a High-Strength Steel Bar
Direct tension analysis results (1 MPa = 145.03 Psi; 1 mm = 0.03937 in.).
Bar size material properties | R–O parameters | ρ | Initial crack series | Second crack series | Third crack series | |||
---|---|---|---|---|---|---|---|---|
f_{ s } (MPa) | s (mm) | f_{ s } (MPa) | s (mm) | f_{ s } (MPa) | s (mm) | |||
#4 f_{ u } = 1,200 MPa f_{ y } = 965 MPa | A = 0.004 B = 1,186 C = 2.8 | 0.02 | 207 | 159 | 227 | 79 | nac | |
0.015 | 262 | 159 | 289 | 79 | nac | |||
0.01 | 386 | 318 | 469 | 159 | nac | |||
0.0075 | 503 | 318 | 613 | 159 | nac | |||
0.005 | 737 | 635 | 923 | 318 | nac | |||
0.0035 | 1,034 | 635 | nac | |||||
#6 f_{ u } = 1,110 MPa f_{ y } = 841 MPa | A = 0.0203 B = 1,365 C = 2.4 | 0.02 | 207 | 159 | nac | |||
0.015 | 262 | 318 | 310 | 159 | nac | |||
0.01 | 386 | 318 | 441 | 159 | nac | |||
0.0075 | 503 | 635 | 620 | 318 | nac | |||
0.005 | 730 | 635 | 910 | 318 | nac | |||
0.0035 | 1,027 | 1,270 | nac | |||||
#8 f_{ u } = 1,069 MPa f_{ y } = 820 MPa | A = 0.0554 B = 1,550 C = 2.9 | 0.02 | 207 | 318 | 227 | 159 | nac | |
0.015 | 262 | 318 | 289 | 159 | nac | |||
0.01 | 379 | 635 | 462 | 318 | nac | |||
0.0075 | 496 | 635 | 613 | 318 | nac | |||
0.005 | 730 | 1,270 | 916 | 635 | nac | |||
0.0035 | 1,027 | 1,270 | nac | |||||
#10 f_{ u } = 1,069 MPa f_{ y } = 820 MPa | A = 0.0554 B = 1,551 C = 2.9 | 0.02 | 207 | 318 | 227 | 159 | nac | |
0.015 | 262 | 318 | 289 | 159 | nac | |||
0.01 | 379 | 635 | 462 | 318 | nac | |||
0.0075 | 496 | 635 | 565 | 635 | 586 | 318 | ||
0.005 | 730 | 1,270 | 923 | 635 | nac | |||
0.0035 | 1,027 | 2,540 | nac |
Crack development and spacing are affected by bar size and the effective concrete area surrounding the reinforcement. As the reinforcing ratio falls, the behavior becomes dominated by a small number of large cracks (Table 1). Whereas at typical flexural reinforcing ratios (0.01 and 0.015), cracking is better distributed. As the reinforcing ratio becomes larger, cracking remains distributed but crack widths may be expected to be more uniform since cracking stresses vary very little. In all cases, for reinforcing ratio ρ = 0.01 and higher, all cracks form at bar stresses below 482 MPa (70 ksi). Consequently, in a concrete section having a reinforcing ratio ρ = 0.01 or higher, regardless of steel grade, the crack width and crack spacing are the same. Using higher strength bars allow higher stresses to develop in the steel, but additional cracks are only likely to form at lower reinforcing ratios.
Based on Fig. 6 for ρ ≤ 0.02, it can be concluded that through reinforcing bar stresses of 496 MPa, average crack widths (it is only possible to consider average crack widths in an analytical context) remain below 0.43 mm (0.017 in.) for all but the largest bars considered (#10). The results were relatively insensitive to changes in reinforcing ratio.
4.2 Experimentally Observed Crack Widths
Details of flexural beam specimens F1–F6 (Shahrooz et al. 2011).
F1 | F2 | F3 | F4 | F5 | F6 | |
---|---|---|---|---|---|---|
A1035 longitudinal steel | ||||||
Lower layer | 4 #5 | 4 #6 | 4 #5 | 4 #5 | 4 #6 | 4 #5 |
Second layer | 2 #5 | 2 #6 | n.a. | 4 #5 | 4 #6 | 2 #5 |
ρ = A_{ s }/bd | 0.012 | 0.016 | 0.007 | 0.016 | 0.023 | 0.012 |
f_{ y } (0.2 % offset) (MPa) | 897 | 839 | 897 | 890 | 926 | 890 |
R–O parameters | ||||||
A | 0.0145 | 0.0203 | 0.0145 | 0.0145 | 0.0130 | 0.0145 |
B | 1,282 | 1,282 | 1,282 | 1,282 | 1,282 | 1,282 |
C | 2.5 | 2.4 | 2.5 | 2.5 | 2.5 | 2.5 |
f_{ c }′ (MPa) | 89 | 89 | 89 | 114 | 112 | 116 |
Specimen cross sections | ||||||
Specimen elevation |
Figure 7a provides the average crack widths measured from all cracks in the 1,016 mm (40 in.) long constant moment region (see Table 2). Figure 7b provides the maximum crack width measured in this region. The ratio of maximum to average measured crack widths for all specimens at all stress levels is 1.8, consistent with available guidance for this ratio, which tends to range between 1.5 and 2.0 (Chowdhury and Loo 2001). In all cases, the ratio of maximum to average crack width falls with increasing bar stress. At approximately 248 MPa (36 ksi), this ratio is 1.7, falling to 1.6 at 414 MPa (60 ksi), and 1.5 at 496 MPa (72 ksi).
The data shown in Fig. 7 clearly show that at rational service load levels (f_{ s } < 496 MPa 72 ksi), average crack widths are all below the present AASHTO de facto limit of 0.43 mm (0.017 in.). Indeed, with the exception of beam F2, maximum crack widths also fall below this threshold through bar stresses of 496 MPa (72 ksi). Crack width is largely unaffected by the reinforcing ratio within the range considered. It is noted that all 305 mm (12 in.) wide beams had four bars [#5 (15.9 mm) or #6 (19 mm)] in the lowermost layer; thus, crack control reinforcing would be considered excellent for these beams.
Considering the measured crack widths in this experimental study, it appears that the existing equations are inherently conservative. This conservativeness allows present specifications to be extended to the anticipated higher service level stresses associated with the use of high strength reinforcing steel.
5 Conclusions
Based on the results of flexural tests conducted as part of a related study, crack widths at service load levels were evaluated and found to be within presently accepted limits, and were predictable using current ACI (2011) or AASHTO (2010) provisions. A limitation on service-level stresses of f_{ s } ≤ 414 MPa (60 ksi) is recommended; this is consistent with a related recommendation that f_{ y } ≤ 689 Mpa (100 Ksi) (Shahrooz et al. 2011).
Based on a parametric study on crack widths, it is shown that crack development and spacing are affected by bar size and the effective concrete area surrounding the reinforcement. As the reinforcing ratio falls, the behavior becomes dominated by a small number of large cracks. Whereas for typical reinforcing ratios (0.01 and 0.015), cracking occurs in a more progressive manner and is better distributed, and hence some variation in crack width along the member should be expected. As the reinforcing ratio becomes larger, cracking remains distributed but crack widths may be expected to be more uniform since cracking stresses vary very little. In all cases considered, for reinforcing ratios ρ = 0.01 and higher, cracks form at bar stresses below 482 MPa (70 ksi). Consequently, in a concrete section with reinforcing ratio ρ = 0.01 or higher, regardless of reinforcing grade, the crack width and crack spacing will be similar.
Based on this study, it can be concluded that through reinforcing bar stresses of 496 MPa (72 ksi), average crack widths remain below 0.43 mm (0.017 in.) for cases having ρ < 0.02 and for all but the largest bars considered [#10 (32 mm)]. The results were relatively insensitive to changes in reinforcing ratio. These results were confirmed by comparison to available experimental data. The ratio of maximum to average crack width was observed to be slightly less than that commonly associated with conventional 414 MPa (60 ksi) reinforcing steel. Additionally, this ratio decreased at higher stress levels.
Declarations
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Authors’ Affiliations
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