# A microstructure based strength model for slag blended concrete with various curing temperatures.

1. IntroductionGranulated slag from metal industries is a steel industrial byproduct and can be used as a mineral admixture to produce normal and high strength concrete. It is broadly recognized that slag blended concrete has many advantages, including lower permeability, better chloride resistance, and higher strength at later ages. In addition, economics (lower cement requirement), energy, and environmental considerations can be achieved by using slag blended concrete [1,2].

Compressive strength is the most important property of hardened concrete; other properties such as tensile strength, flexural strength, elasticity modulus, water tightness, and durability all are related to compressive strength closely. The compressive strength of slag blended concrete generally relates to materials properties, such as water to binder ratios and slag replacement ratios, and curing conditions, such as curing temperatures. Many experimental investigations have been done about strength development of slag blended concrete. Ramezanianpour and Malhotra [3] found that, for moist curing conditions, when slag replaces cement at 25% of total binder content, the early-age strength is lower than that of control concrete and the late age is higher than that of control concrete. While for slag replacing cement at 50%, until the age of 90 days, the compressive strength is still lower than that of control concrete. Luan et al. [4] found when the slag content is less than 50% of total binder content, as slag content increases, the strength of concrete will increase correspondingly. After around 50% of the total binder content, the further addition of GGBS does not improve the compressive strength. So 50% of total binder content is the optimum content of slag. Eren [5] found that with the increasing of curing temperature, compared with that of standard curing at 20[degrees]C, the early-age strength of slag blended concrete will increase. However, the late age strength will decrease.

Compared with abundant experimental study on strength development of slag blended concrete [3-5], theoretical models are very limited. To estimate compressive strength of concrete containing different supplementary cementing materials, Papadakis et al. [6,7] proposed an efficiency factor of the SCM in an SCM-concrete. This efficiency factor describes the relative reactivity of SCM to cement. However, it should be noticed that Papadakis' model [6, 7] is not a kinetic model and only valid for standard curing condition. Ishida et al. [8] proposed a kinetic microstructure model to simulate cement hydration and slag reaction. The strength development is evaluated using reaction degrees of cement and slag. This kinetic model is valid for concrete with larger slag contents (60% slag of total binder contents). But the effect of curing temperature on strength development is not considered in Ishida et al.'s study [8]. On the other hand, Brooks and Al-Kaisi [9] and Barnett et al. [10] proposed maturity functions to model the strength development of slag blended concrete at elevated temperatures. The ultimate strength becomes lower when curing temperature increases. However, it should be noticed that maturity function method belongs to a macroregression method. Cement hydration, slag reaction, and evolution of microstructure of hardening concrete are not detailedly considered in maturity function method [9,10].

The development of mechanical properties of slag blended concrete relates to cement hydration and slag reaction. To overcome the weak points of current models [6-10], this paper puts forward a numerical procedure to simulate cement hydration, slag reaction, microstructure development, and strength development of slag blended concrete. The proposed procedure can reproduce strength crossover phenomenon of slag blended concrete with low curing temperatures and high curing temperatures. The proposed model is valid for slag blended concrete with different slag contents, different isothermal curing temperatures, and time varying curing temperatures.

2. Modeling of Hydration of Cement-Slag Blends

The development of concrete properties closely relates to hydration process. For hardening concrete, heat properties, mechanical properties, and chemical properties develop accompanied with cement hydration. For hardened concrete, compositions of hydration reaction products and capillary pore structures closely relate to degree of hydration. Hence modeling of hydration process is important for evaluating concrete properties. For cement-slag blends, cement hydration and slag reaction will occur simultaneously. To model hydration of cement-slag blends, we propose cement hydration model, slag reaction model, and interaction model between cement hydration and slag reaction.

2.1. Portland Cement Hydration Model. Tomosawa [11] measured the isothermal heat evolution rate of Portland cement paste. He found that cement hydration generally consists of three processes, that is, initial dormant process, phase-boundary reaction process, and diffusion process. Tomosawa [11] also presents a shrinking-core model to simulate the hydration of Portland cement. However, because Tomosawa's model does not consider the influence of capillary water concentration on cement hydration, this model is valid only for low strength concrete. For high strength concrete, due to the lower water to binder ratio, at late ages, capillary water concentration will significantly decrease, and rate of cement hydration will decrease correspondingly. Wang [12] revised Tomosawa's model [11] to consider the effect of capillary water concentration on hydration. The revised equation is shown as follows [12]:

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII], (1a)

[alpha] = [[summation].sup.4.sub.i=1][[alpha].sub.i][g.sub.i]/ [[summation].sup.4.sub.i=1][g.sub.i], (1b)

where [[alpha].sub.i] (i = 1, 2, 3, and 4) denotes reaction degree of mineral compound of cement [C.sub.3]S, [C.sub.2]S, [C.sub.3]A, and [C.sub.4]AF, respectively; a denotes the degree of cement hydration; kd is the reaction coefficient in the initial dormant period; De is the effective diffusion coefficient of water through the C-S-H gel; [k.sub.ri] is the reaction coefficient of boundary reaction process; v denotes the stoichiometric ratio by mass of water to cement (=0.25); [w.sub.g] denotes the physically bound water in C-S-H gel (=0.15); [[rho].sub.w] denotes the density of water; pc denotes the density of the cement; [C.sub.w-free] denotes the amount of water at the exterior of the C-S-H gel; [r.sub.0] denotes the radius of unhydrated cement particles; [S.sub.w] denotes the effective surface area of the cement particles in contact with water; and [S.sub.0] denotes the total surface area if the surface area develops unconstrained.

As shown in (1b), reaction degree of cement a can be calculated from the weight fraction of mineral compound [g.sub.i] and reaction degree of mineral compound [[alpha].sub.i].

During initial dormant period, the formation of initial impermeable layer will lower rate of hydration, and the destruction of this impermeable layer will increase the rate of hydration. The reaction coefficient [k.sub.d] in the initial dormant period can be determined as follows:

[k.sub.d] = [B/[[alpha].sup.1.5]] + C[[alpha].sup.3], (2)

where B describes the rate of the initial shell formation and C describes the rate of the initial shell decay.

The effective diffusion coefficient of water De relates to the tortuosity of the gel pores and the radii of gel pores in reaction products. [D.sub.e] can be described as a function of hydration degree as follows:

[D.sub.e] = [D.sub.e0] ln(1/[alpha]). (3)

The amount of water in the capillary pores [C.sub.w-free] is determined as a function of hydration degree as shown in

[C.sub.w-free] = [W.sub.0] - 0.4 * [alpha] * [C.sub.0]/[W.sub.0], (4)

where [C.sub.0] and [W.sub.0] are the mass of cement and water in the mix proportion, respectively. The term [W.sub.0] - 0.4 * [alpha] * [C.sub.0] in numerator considers the consumption of capillary water from cement hydration.

The influence of curing temperatures on reaction coefficients is described using Arrhenius's law as shown in

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII], (5)

where [[beta].sub.1], [[beta].sub.2], E/R, and [[beta].sub.3] represent temperature sensitivity coefficients and [B.sub.20], [C.sub.20], [k.sub.ri20], and [D.sub.e20] denote the values of B, C, [k.sub.ri], and D, at 20[degrees]C, respectively.

Using degree of reactions of mineral compounds of cement [13], the parameters of hydration model are calibrated and are shown in Table 1. Based on this Portland cement hydration model, Wang [12] evaluates chemically bound water, adiabatic temperature rising, and mechanical properties of high strength concrete incorporating Portland cement with different mineral compositions and different Blaine surfaces. The prediction results generally agree with experimental results.

2.2. Reaction Model of Slag. Maekawa et al. [14] measured the isothermal heat evolution rate of cement-slag paste. They found that the kinetic reaction process of slag is similar to that of cement. Slag reaction also consists of initial dormant period, boundary reaction process, and diffusion-controlled process. On the other hand, slag presents cementitious behavior (latent hydraulic activity) and pozzolanic behavior (reaction with lime). Slag reaction relates to capillary water contents and calcium hydroxide contents. Considering these points, we proposed that reaction of slag can be described as follows:

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII], (6a)

[k.sub.dSG] = [[B.sub.SG]/[([[alpha].sub.SG]).sup.1.5]] + [C.sub.SG] * [([[alpha].sub.SG]).sup.3], (6b)

[D.sub.eSG] = [D.sub.eSG0] * ln(1/[[alpha].sub.SG]), (6c)

where [[alpha].sub.SG] denotes the degree of reaction of slag; mCH(i) denotes the calcium hydroxide mass; P denotes the mass of slag in the mixture proportion; [W.sub.cap] denotes the mass of capillary water; [v.sub.SG] denotes the stoichiometric ratio of mass of CH to slag; [r.sub.SG0] denotes the radius of the slag particle; [[rho].sub.SG] denotes the density of the slag; [k.sub.dSG] denotes the reaction rate coefficient in the dormant period ([B.sub.SG] and [C.sub.SG] are coefficients); [D.sub.eSG0] denotes the initial diffusion coefficient; and krSG denotes the reaction rate coefficient. In (6a), the term [m.sub.CH](t)/P considers the pozzolanic behavior of slag, and the term [W.sub.cap]/[W.sub.0] considers the latent hydraulic activity of slag.

The influence of temperature on slag reaction is described by the Arrhenius law as follows:

[B.sub.SG] = [B.sub.SG20] exp([[beta].sub.1SG]([1/T] - [1/293])), (6d)

[C.sub.SG] = [C.sub.SG20] exp([[beta].sub.2SG]([1/T] - [1/293])), (6e)

[D.sub.eSG0] = [D.sub.eSG20] exp ([[beta].sub.3SG] ([1/T] - [1/293])), (6f)

[K.sub.rSG] = [k.sub.rSG20] exp (-[E.sub.SG]/R([1/T] - [1/293])), (6g)

where [B.sub.SG20], [C.sub.SG20], [D.sub.eSG20], and [k.sub.rSG20] denote the values of [B.sub.SG], [C.sub.SG], [D.sub.eSG0], and [k.sub.rSG] at 20[degrees]C, respectively and [[beta].sub.2SG], [[beta].sub.3SG], and [E.sub.SG]/R denote the temperature sensitivity coefficients of [B.sub.SG], [C.sub.SG], [D.sub.eSG0], and [k.sub.rSG], respectively. The temperature sensitivity coefficients of slag can be regressed by using reaction degree of slag at different curing temperatures [11, 14].

In addition, besides chemical reaction, the addition of slag also presents dilution effect [12]. When slag is used as a mineral admixture, water to cement ratio will increase. For high strength concrete with a lower water to binder ratio, this dilution effect will be significant. In this paper, this dilution effect is considered through [C.sub.0]/[W.sub.0] term in (4).

2.3. Interaction Model between Cement Hydration and Slag Reaction. Maekawa et al. [14] systematically analyzed the chemical, thermal, and mechanical properties of slag blended concrete. For the stoichiometry of slag reaction, Maekawa et al. summarized that when 1g slag reacts, 0.22 g calcium hydroxide will be consumed; 0.30 g chemically bound water and 0.15 g physically bound water will be produced.

Considering the production of calcium hydroxide from cement hydration and the consumption of calcium hydroxide from slag reaction, the amounts of calcium hydroxide in cement-slag can be determined as follows:

CH = [RCH.sub.CE] * [C.sub.0] * [alpha] - [RCH.sub.SG] * [[alpha].sub.SG] * P, (7)

where [RCH.sub.CE] is the mass of produced calcium hydroxide from cement hydration and [RCH.sub.SG] is the mass of reacted calcium hydroxide in slag reaction.

Chemically bound water relates to both cement hydration and slag reaction. The chemically bound water contents can be determined as follows:

[W.sub.cbm] = V * [C.sub.0] * [alpha] + [RCW.sub.SG] * [[alpha].sub.SG] * P, (8)

where [RCW.sub.SG] is the mass of chemically bound water in slag reaction.

In cement-slag blends, capillary water will be consumed from cement hydration and slag reaction. The capillary water contents can be calculated as follows:

[W.sub.cap] = [W.sub.0] - 0.4 * [C.sub.0] * [alpha] - [RCW.sub.SG] * [[alpha].sub.SG] * P - [RPW.sub.SG] * [[alpha].sub.SG] * P, (9)

where [RPW.sub.SG] is the mass of gel water in the slag reaction.

Summarily, the proposed blended cement hydration model considers both cement hydration and slag reaction. The influences of water to binder ratios, slag replacement ratios, and curing temperatures on hydration are taken into account. The interactions between cement hydration and slag reaction are considered through calcium hydroxide content and capillary water contents. The reaction coefficients in hydration model are not changed with concrete mixing proportions. When water to binder ratio or slag replacement alters, these parameters of slag do not change.

2.4. Calibration and Parameter Study of Hydration Model. Iyoda et al. [15] measured slag reaction degrees in cementslag paste at different curing temperatures (5[degrees]C, 20[degrees]C, and 40[degrees]C) and slag substitution ratios (42% and 67% mass percent). The water to binder ratio of paste is 0.5. By using a selective dissolution method, the reaction degree of slag was measured at different curing ages. Using experimental results of reaction degree of slag [15], the reaction coefficients of slag are calibrated and shown in Table 2.

As shown in Figure 1, the prediction results generally agree with experimental results. Figure 2 shows parameter study about reaction degree of slag. The influences of slag replacement ratios, water to binder ratios, curing temperatures, and Blaine surface (fineness of slag) on reaction degree of slag are presented. As shown in Figure 2(a), with a reduction of the replacement level of slag, the alkaline activating effect of the cement would be greater, so that the reactivity of slag will increase. As shown in Figure 2(b), with an increase of water to binder ratio, there is more space available for hydration products to form; hence the reactivity of slag increases correspondingly. As shown in Figure 2(c), due to the increasing of curing temperatures, slag reaction will accelerate. As shown in Figure 2(d), with an increase of Blaine surface, slag particle will be much finer and the reactivity will be enhanced.

Zheng et al. [16] studied the evolution of calcium hydroxide contents in cement-slag blends. The water to binder ratio is 0.5, slag replacement ratios vary between 0.3 and 0.6, and the cement-slag paste specimens were cured at 20[degrees]C. The amount of calcium hydroxide was estimated from the weight loss at 450-550[degrees]C using TG-DTA method at different curing ages. Using the proposed slag blended cement hydration model and reaction coefficients of cement and slag, the evolution of calcium hydroxide is calculated and shown in Figure 3. In the hydration of ordinary Portland cement, the mass of calcium hydroxide will increase before reaching a steady state. In the hydration of cement-slag blends, the evolution of the CH mass depends on two factors: the cement hydration which produces CH and the reaction of slag that consumes CH. When slag replaces cement to a high percentage, the CH content may pass through a maximum level and then decrease.

The flowchart of modeling is summarized in Figure 4. At each time step, cement hydration degree and slag reaction degree are calculated. The capillary water contents, calcium hydroxide contents, and chemically bound water contents are calculated considering contributions from both cement hydration and slag reaction. Furthermore, using reaction degrees of cement and slag, volumetric stoichiometries of cement hydration and slag reaction, and mixing proportions of slag blended concrete, the gel-space ratio [17-20] and compressive strength development of hardening concrete can be calculated [17-20].

3. Evaluation of Compressive Strength Development of Hardening Slag Blended Concrete

3.1. Strength Development Model of Hardening Concrete. Wang [17, 18], Lam et al. [19], and Oh and Cha [20] proposed that the compressive strength of concrete depends on the gel/space ratio determined from degree of cement hydration and water to cement ratio. A gel/space ratio is defined as the ratio of the volumes of cement reaction products to the sum of the volumes of the hydrated cement and of the capillary pores. For cement-slag blends, the reaction products of binders consist of cement hydration products and slag reaction products. The gel/space ratio of cement-slag blends is given by

[x.sub.fc] = v(T)(1/[rho])[alpha][C.sub.0] + [v.sub.SG](T)(1/[[rho].sub.SG])[[alpha].sub.SG]P/ (1/[rho])[alpha][C.sub.0] + (1/[[rho].sub.SG])[[alpha].sub.SG]P + [W.sub.0], (10a)

where [x.sub.fc] is the gel/space ratio of blended cement pastes, v(T) is the volume of hydration products of 1 unit volume cement, and vSG(T) is the volume of reaction products of 1-unit volume slag.

Wang [18] and van Breugel [21] proposed that, with the increasing of curing temperature, the thickness of reaction products layer decreases. Hence the values of v(T) and [v.sub.SG](T) are not constant, but the decreasing functions of curing temperature are as follows [18, 21]:

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII], (10b)

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII]. (10c)

As shown in (10b) and (10c), the volume change of slag is larger than the anhydrous cement. This may be partially due to the lower density of slag hydration products and may indicate that slag reaction products are more effective in filling pores.

The development of compressive strength of Portland cement concrete can be calculated using Powers' strength theory as follows [18-21]:

[f.sub.c](t) = A[x.sub.fc.sup.n], (10d)

where [f.sub.c](t) is the compressive strength of concrete, A is the intrinsic strength of the material, and n is the strength exponent.

Powers' strength theory (see (10d)) is generally valid for Portland cement concrete. For slag blended concrete, due to the coexistence of cement hydration and slag reaction, the intrinsic strength of the material A and strength exponent n will relate to both cement hydration and slag reaction. For slag blended concrete with different slag contents, the intrinsic strength of the material A and strength exponent n will be different. Hence Powers' strength theory (see (10d)) cannot be used directly to evaluate strength development of slag blended concrete.

To improve Powers' strength theory (see (10d)) for slag blended concrete, we simply assume that the intrinsic strength of the material A and strength exponent n can be expressed as a function of weight fractions of cement ([C.sub.0]/ ([C.sub.0] + P)) and slag (P/([C.sub.0] + P)) in the mixing proportion as follows:

A = a1 * [[C.sub.0]/[C.sub.0] + P] + a2 * [P/[C.sub.0] + P], (10e)

n = b1 * [[C.sub.0]/[C.sub.0] + P] + b2 * [P/[C.sub.0] + P], (10f)

where coefficients a1 and a2 in (10e) represent the contributions of cement and slag to the intrinsic strength of materials, respectively, the units of a1 and a2 are MPa, and the coefficients b1 and b2 in (10f) represent the contributions of cement and slag to strength exponent, respectively. For Portland cement concrete, the weight fractions of slag are zero, and (10e) and (10f) are the same as Powers' strength theory (see (10d)).

Wang [17,18] and Eren [5] found that, for low temperature casting, microstructure of the hydrated cement paste will be uniform, and the strength will be higher. Hence it is assumed that the ultimate strength of concrete (similar to intrinsic strength of concrete) is a decreasing function of curing temperature as follows:

A = [A.sub.20] * [e.sup.-c*(T-20)] (10g)

where [A.sub.20] is the intrinsic strength of concrete cured at 20[degrees] C and and strength reduction coefficient c in the exponential part means that, with an increase of the curing temperature, the intrinsic strength of concrete A will decrease.

For hardening concrete, the development of compressive strength relates to some competing factors: with the increasing of curing temperature, the rate of cement hydration and slag reaction will increase (see (5) and (6d) to (6g)). Consequently, with the increase of curing temperatures, at a certain age, compressive strength of concrete will increase. On the other hand, when curing temperature increases, the ratio between volume of reaction products and that of reacted binders will decrease (see (10b) to (10c)). In addition, when curing temperature increases, the ultimate strength of concrete will decrease (see (10g)). These factors will weaken the increasing trend of compressive strength. Summarily, based on the proposed blended cement hydration model and strength development model, we can model the strength crossover phenomenon for concrete with different curing temperatures.

3.2. Verifications of Proposed Model. Brooks and Al-Kaisi [9] studied the compressive strength development of slag blended concrete at elevated temperatures. The properties of binders are shown in Table 3. The first concrete was an OPC control mix having cement: fine aggregate: coarse aggregate mass proportions of 1: 1.62:2.49 with a water-cement ratio of 0.42. The second and third concretes had 50 and 70 percent of the mass of OPC replaced by equal masses of slag, respectively, with the same aggregate proportions and water-cementitious-materials ratio as the control concrete.

For each concrete, cubes were cast at 20[degrees]C cured in water tanks under two conditions: isothermal curing, where cubes were subjected to temperatures of 20, 40, and 47[degrees]C; and heat-cycled curing, where the cubes were subjected to a controlled ascending temperature rise, and on reaching the peak temperature, the control system was switched off, and the cubes were allowed to cool to the ambient temperature. The amount of inhibitions of capillary water from surrounding moist curing related to the chemical shrinkage of hardening paste [17, 18].

Using experimental results of compressive strength of concrete cured as 20[degrees]C, the intrinsic strength coefficients in (10e) and strength exponent in (10f) can be calibrated as a1 = 103, a2 = 123, b1 = 2.11, and b2 = 2.44 (these coefficients do not vary with slag replacement ratio). As shown in Figure 5, for concrete incorporating 50% slag, the early-age strength is lower than that of Portland cement concrete, and late age strength will surpass that of control concrete. Contrastively, for concrete incorporating 70% slag, both early-age strength and late age strength are lower than those of control concrete. This is because the reactivity of slag decreases with the increasing of slag replacement ratio (shown in Figure 1).

The phase volume fractions of hardening slag-cement paste are shown in Figure 6 (water to binder ratio is 0.5, slag replacement ratio is 0.5, and curing temperature is 20[degrees]C). As shown in this figure, with the proceeding of hydration reactions, the volumes of unreacted cement and slag decrease, the volumes of reaction products increase, and the volume of capillary pore decrease. At early-age, hydration reactions proceed quickly, and at late age the reactions rate becomes slower.

Figure 7 presents parameter analysis about compressive strength development of concrete incorporating different slag contents. The water to binder is 0.42 and curing temperature is 20[degrees] C, and the curing ages vary from 1 day to 360 days. The vertical axis represents the strength ratio of slag blended concrete to OPC at the same age. At an early age of 1 day, strength decreases as the slag ratio increases. This may be attributed to the lower reaction degree of slag. As the age increases, for concrete with higher slag ratios, the strength increases faster, and at a long-term age of 360 days, the maximum value of strength lies in the range of 30%-40% slag ratios. However, with regard to a slag ratio higher than 40%, due to the lower reaction degree of slag, the ultimate strength ratio is less. Hence, for the binders used in this study, the optimum replacement ratio of slag is about 40%. On the other hand, when the replacement ratio of slag is higher than 60%, even at the late age of 360 days, the strength of slag concrete is yet lower than that of OPC due to the lower reaction degree of slag and lack of reaction products from slag reaction. So when the equivalent strength is necessary, the slag contents in binders should be less than 60%.

Using experimental results of strength development of slag blended concrete at different isothermal curing temperatures, we can calibrate the strength reduction coefficient c in (10g). For OPC concrete, 50% slag blended concrete, and 70% slag blended concrete, the values of strength reduction coefficient b are 0.014, 0.009, and 0.002 respectively. It is noticed that, with the increasing of curing temperature, the compressive strength of slag blended concrete decreases much slower than that of Portland cement concrete. This may be because of pore-size refinement and grain-size refinement effects from slag reactions [18]. The formation of slag reaction products can fill the large capillary voids and average pore size can be reduced. Also, due to the reaction between calcium hydroxide and slag, calcium hydroxide large grains can be decreased.

As shown in Figure 8, the proposed model can reproduce crossover phenomenon for compressive strength development of concrete at different curing temperatures. With the increasing of curing temperature, cement hydration and slag reaction will accelerate, and early-age strength of concrete will increase correspondingly. On the other hand, the increasing of curing temperature will make reaction products of cement and slag distribute inhomogeneously, larger capillary pores in concrete will increase, and the late age strength of concrete will reduce.

In addition, as shown in Figure 8(a) (OPC concrete) and Figure 8(c) (70% slag concrete), at late age, when the curing temperature is 20[degrees]C, the compressive strength of OPC concrete is higher than that of 70% slag concrete; when the curing temperature is 40[degrees]C, the compressive strength of 70% slag concrete is comparable with that of OPC concrete; and when the curing temperature is 47[degrees] C, the compressive strength of 70% slag concrete is higher than that of OPC concrete. This is due to pore-size refinement and grain-size refinement effects from slag reactions. For concrete with elevated curing temperatures, strength of slag blended concrete decreases much slower than that of Portland cement concrete.

Figure 9 presents holistic comparison between evaluation results and experimental results. The evaluation results generally agree with experimental results. However, at very early age, the analysis results are slightly higher than that of experimental results. This is because of the ignorance of compressive strength threshold in the analysis process (when cement hydration degree is less than this threshold degree of hydration, compressive strength is zero).

For hardening concrete with time varying curing temperature, by using the differential expression of (10d), the compressive strength development can be calculated. The curing temperature histories are shown in Figure 10. This curing temperature history is similar to actual temperature history of hardening mass concrete in construction site. The curing temperature of concrete first increases at a high rate; after reaching peak temperature, the temperature decreases slowly. As shown in Figure 11, the proposed model can reproduce the compressive strength development of control concrete and slag blended concrete with a time varying curing temperature. For the temperature history shown in Figure 11, the late strength of 70% slag blended concrete (Figure 11(b)) is slightly higher than that of control Portland cement concrete (Figure 11(a)). While for 20[degrees]C curing temperature, as shown in Figures 5 and 7, the compressive strength of 70% slag concrete is always lower than that of control concrete. This is because the strength reduction coefficient of OPC is much higher than that of slag blended concrete. Hence, with the increasing of curing temperature, OPC concrete shows more strength loss than that of slag blended concrete.

In addition, it should be noticed that the proposed model is generally valid for normal strength concrete. For ultrahigh strength concrete, aggregate will contribute to compressive strength. To accurately evaluate strength development of hardening concrete, composite model which simulates interactions between cement paste and aggregate is necessary [1921].

4. Conclusions

This paper presents a numerical procedure to simulate cement hydration, slag reaction, microstructure development, and strength development of slag blended concrete. Cement hydration model and slag reaction model are simulated separately. The interactions between cement hydration and slag reaction are considered through available capillary water contents and calcium hydroxide contents in cement-slag blends system. Furthermore, using reaction degrees of cement and slag, volumetric stoichiometries of cement hydration and slag reaction and mixing proportions of slag blended concrete, the gel-space ratio and strength development of hardening concrete are determined.

The proposed model considers both strengthening factors and weakening factors involved in strength development process of slag blended concrete: due to the increase of curing temperature, cement hydration and slag reaction are accelerated, the ratios between the volume of reaction products and that of reacted binders decrease, and the ultimate strength of concrete is reduced. The proposed procedure can reproduce strength crossover phenomenon of hardening concrete with low curing temperatures and high curing temperatures. The proposed model is valid for concrete with different slag contents, different curing temperatures, and time varying temperature history.

http://dx.doi.org/10.1155/2016/1738417

Competing Interests

The authors declare that they have no competing interests.

Acknowledgments

This research was supported by a grant (13SCIPA02) from Smart Civil Infrastructure Research Program funded by Ministry of Land, Infrastructure and Transport (MOLIT) of Korea Government and Korea Agency for Infrastructure Technology Advancement (KAIA).

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Li-Na Zhang, (1) Wang Xiao-Yong, (1) and Kyung-Taek Koh (2)

(1) Department of Architectural Engineering, Kangwon National University, Chuncheon-Si 200-701, Republic of Korea

(2) Structural Engineering Research Division, Korea Institute of Construction Technology, Goyang-Si 411-712, Republic of Korea

Correspondence should be addressed to Wang Xiao-Yong; wxbrave@kangwon.ac.kr

Received 7 October 2015; Accepted 24 November 2015

Academic Editor: Yuyin Wang

Caption: Figure 1: Reaction degree of slag with different slag replacement ratios and curing temperatures: (a) cement-slag paste with 42% slag; (b) cement-slag paste with 67% slag.

Caption: Figure 2: Parameter study of reaction degree of slag: (a) slag replacement ratios; (b) water to binder ratios; (c) curing temperatures; and (d) fineness of slag (Blaine surface).

Caption: Figure 3: Evaluation of calcium hydroxide contents in cement-slag blends (water to binder ratio 0.5).

Caption: Figure 4: Flowchart of modeling.

Caption: Figure 5: Evaluation of compressive strength development of slag blended concrete at 20[degrees] C curing temperature.

Caption: Figure 6: Phase volume fractions of hardening slag-cement paste (water to binder ratio 0.5, slag replacement ratio 0.5).

Caption: Figure 7: Effects of slag additions on strength development of concrete.

Caption: Figure 8: Strength development of concrete at different curing temperatures.

Caption: Figure 9: Comparsion between analysis results and experimental results.

Caption: Figure 10: Temperature history of hardening concrete.

Caption: Figure 11: Strength development of concrete at time varying curing temperature.

Table 1: Coefficients of cement hydration model. [MATHEMATICAL [MATHEMATICAL EXPRESSION NOT EXPRESSION NOT REPRODUCIBLE REPRODUCIBLE [B.sub.20] [C.sub.0] IN ASCII] IN ASCII] (cm/h) (cm/h) (cm/h) (cm/h) 8.1 x [10.sup.-9] 0.02 9.0 x [10.sup.-6] 2.7 x [10.sup.-7] [MATHEMATICAL [MATHEMATICAL EXPRESSION NOT EXPRESSION NOT REPRODUCIBLE REPRODUCIBLE [B.sub.20] IN ASCII] IN ASCII] (cm/h) (cm/h) (cm/h) 8.1 x [10.sup.-9] 1.4 x [10.sup.-6] 6.8 x [10.sup.-8] [MATHEMATICAL EXPRESSION NOT REPRODUCIBLE [B.sub.20] IN ASCII] [[beta].sub.1] [[beta].sub.2] (cm/h) (cm2/h) (K) (K) 8.1 x [10.sup.-9] 8.6 x [10.sup.-10] 1000 1000 [B.sub.20] [[beta].sub.3] h/R (cm/h) (K) (K) 8.1 x [10.sup.-9] 7500 5400 Table 2: Coefficients of slag reaction model. [B.sub.20SG] [C.sub.SG20] [K.sub.rSG20] (cm/h) (cm/h) (cm/h) 8.9 x [10.sup.-9] 0.1 1.0 x [10.sup.-5] [B.sub.20SG] [D.sub.eSG20] [[beta].sub.1SG] (cm/h) ([cm.sup.2]/h) (K) 8.9 x [10.sup.-9] 1.9 x [10.sup.-9] 1000 [B.sub.20SG] [[beta].sub.2SG] [[beta].sub.3SG] (cm/h) (K) (K) 8.9 x [10.sup.-9] 1000 5000 [B.sub.20SG] [E.sub.SG]/R (cm/h) (K) 8.9 x [10.sup.-9] 7000 Table 3: Properties of binders. Material Oxide, percent CaO Si[O.sub.2] [Al.sub.2][O.sub.3] OPC 65.8 20.5 5.8 Slag 40.4 36.1 10.8 Material Oxide, percent [Fe.sub.2][O.sub.3] MgO S[O.sub.3] [K.sub.2]O OPC 2.5 1.2 2.3 0.6 Slag 0.4 9.5 0.3 0.5 Material Oxide, percent Specific surface area [Na.sub.2]O MnO Ti[O.sub.2] ([m.sup.2]/kg) OPC 0.3 0.1 0.2 391 Slag 0.3 0.6 0.7 412

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Title Annotation: | Research Article |
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Author: | Zhang, Li-Na; Xiao-Yong, Wang; Koh, Kyung-Taek |

Publication: | Advances in Materials Science and Engineering |

Article Type: | Report |

Date: | Jan 1, 2016 |

Words: | 6289 |

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