2.1 Governing equations

We solve the conservation equations for mass, momentum, and energy in the Boussinesq approximation:

(2.1a ) $$\begin{eqnarray}\displaystyle & \displaystyle \unicode[STIX]{x1D735}\boldsymbol{\cdot }\boldsymbol{u}=0, & \displaystyle\end{eqnarray}$$

(2.1b ) $$\begin{eqnarray}\displaystyle & \displaystyle \frac{\unicode[STIX]{x2202}\boldsymbol{u}}{\unicode[STIX]{x2202}t}+\unicode[STIX]{x1D735}\boldsymbol{\cdot }(\boldsymbol{u}\otimes \boldsymbol{u})=-\unicode[STIX]{x1D735}p+\unicode[STIX]{x1D708}\unicode[STIX]{x1D6FB}^{2}\boldsymbol{u}+b\boldsymbol{k}, & \displaystyle\end{eqnarray}$$

(2.1c ) $$\begin{eqnarray}\displaystyle & \displaystyle \frac{\unicode[STIX]{x2202}b}{\unicode[STIX]{x2202}t}+\unicode[STIX]{x1D735}\boldsymbol{\cdot }(\boldsymbol{u}b)=\unicode[STIX]{x1D705}_{b}\unicode[STIX]{x1D6FB}^{2}b, & \displaystyle\end{eqnarray}$$

$\boldsymbol{u}(\boldsymbol{x},t)$

$(u,v,w)$

$\boldsymbol{x}=(x,y,z)$

$x$

$y$

$z$

$t$

$\boldsymbol{k}=(0,0,1)$

$p$

$b$

$\unicode[STIX]{x1D703}_{v}$

$b\simeq g(\unicode[STIX]{x1D703}_{v}-\unicode[STIX]{x1D703}_{v,0})/\unicode[STIX]{x1D703}_{v,0}$

$\unicode[STIX]{x1D703}_{v,0}$

$\unicode[STIX]{x1D703}_{v}$

$\unicode[STIX]{x1D708}$

$\unicode[STIX]{x1D705}_{b}$

$b$

Figure 1.

Sketch of the barotropic CBL considered in this analysis. The vertical white bars indicate different definitions of the CBL depth, namely, from left to right, the encroachment length scale, $z_{enc}$ , the flux-based height, $z_{i,f}$ , and the gradient-based height, $z_{i,g}$ . The background is a cross-section of the logarithm of the magnitude of the buoyancy gradient from case $Fr_{0}=20$ and $Re_{0}=25$ of table 1 at $z_{enc}/L_{0}\simeq 15$ . (The image only shows the lower $40\,\%$ of the vertical domain.)

Impermeable, no-slip and impermeable, free-slip boundary conditions are applied, respectively, at the bottom and at the top of the domain. Neumann boundary conditions are used for the buoyancy at the bottom, $\unicode[STIX]{x2202}_{z}b=-B_{0}/\unicode[STIX]{x1D705}_{b}$ , and at the top, $\unicode[STIX]{x2202}_{z}b=N_{0}^{2}$ , to maintain fixed constant fluxes. Periodicity is applied at the lateral boundaries. A linear relaxation term acts on the velocity and buoyancy fields inside a sponge layer occupying the upper 15 %–20 % of the computational domain. The reference values of this relaxation term are the initial conditions. The proportionality coefficient of the relaxation term increases quadratically with the distance from the inner limit of the sponge layer, from zero at the inner limit to $N_{0}/(2\unicode[STIX]{x03C0})$ at the outer limit (which coincides with the top of the computational domain).

The initial buoyancy field is defined as

(2.2) $$\begin{eqnarray}b(\boldsymbol{x},0)=b_{ics}\left[1-\text{erf}\left(\frac{\sqrt{\unicode[STIX]{x03C0}}}{2}\frac{z}{\unicode[STIX]{x1D6FF}_{ics}}\right)\right]+N_{0}^{2}z,\end{eqnarray}$$

where $b_{ics}(x_{1},x_{2})=(B_{0}/\unicode[STIX]{x1D705}_{b}+N_{0}^{2})\unicode[STIX]{x1D6FF}_{ics}(x_{1},x_{2})$ is the surface buoyancy and $\unicode[STIX]{x1D6FF}_{ics}$ is the local gradient thickness (Mellado, van Heerwaarden & Garcia Reference Mellado, van Heerwaarden and Garcia2016). A broadband field is constructed by specifying $\unicode[STIX]{x1D6FF}_{ics}(x_{1},x_{2})=\unicode[STIX]{x1D6FF}_{0}[1+\unicode[STIX]{x1D709}(x_{1},x_{2})]$ , with the parameter $\unicode[STIX]{x1D6FF}_{0}$ to be given. The random field $\unicode[STIX]{x1D709}(x_{1},x_{2})$ has a Gaussian power spectral density centred at a spatial frequency $\unicode[STIX]{x1D706}_{0}^{-1}=(4\unicode[STIX]{x1D6FF}_{0})^{-1}$ and with a standard deviation $(6\unicode[STIX]{x1D706}_{0})^{-1}$ , so that there is practically no energy with spatial frequencies below $(2\unicode[STIX]{x1D706}_{0})^{-1}$ . The phase of $\unicode[STIX]{x1D709}$ is random, its mean value is zero and the root-mean-square (r.m.s.) is $\unicode[STIX]{x1D709}_{rms}=0.1$ . The initial velocity field is imposed as

(2.3) $$\begin{eqnarray}\boldsymbol{u}(\boldsymbol{x},0)=U_{0}\left[\text{erf}\left(\frac{\sqrt{\unicode[STIX]{x03C0}}}{2}\frac{z}{\unicode[STIX]{x1D6FF}_{0}}\right)\right]\boldsymbol{i},\end{eqnarray}$$

where $\boldsymbol{i}=(1,0,0)$ . Such a function provides the no-slip boundary condition at the surface and a height-constant velocity in the streamwise direction in the bulk of the domain.

A finite difference method using Cartesian coordinates and a structured grid is employed to solve the governing equations. The discretization of the equations is carried out by sixth-order spectral-like compact schemes for the spatial derivatives (Lele Reference Lele1992) along with a low-storage fourth-order Runge–Kutta scheme to advance in time (Carpenter & Kennedy Reference Carpenter and Kennedy1994). For the compact schemes used in this study, approximately four points per wavelength provide $99\,\%$ accuracy in the transfer function of the derivative operator. For comparison, second-order central schemes need approximately eight points per wavelength to reach $90\,\%$ accuracy, which is the motivation to employ compact schemes despite being computationally more demanding (Lele Reference Lele1992). The pressure-Poisson equation is solved using a Fourier decomposition along the horizontal directions, which results in a set of second-order differential equations along the vertical coordinate (Mellado & Ansorge Reference Mellado and Ansorge2012).

2.2 Dimensional analysis

The sheared CBL described in the previous section is completely governed by the control parameters $\{\unicode[STIX]{x1D708},\unicode[STIX]{x1D705}_{b},B_{0},N_{0},U_{0}\}$ once the turbulent flow has sufficiently forgotten the initial conditions. Hence, three non-dimensional parameters are sufficient to characterize the system. In this work, we take the shear-free limit $U_{0}=0$ as reference and study how entrainment-zone properties change as we gradually increase the wind velocity. Hence, we choose $N_{0}$ and $B_{0}$ to non-dimensionalize the problem, which yields $N_{0}^{-1}$ as the reference time scale,

(2.4) $$\begin{eqnarray}L_{0}\equiv \left(\frac{B_{0}}{N_{0}^{3}}\right)^{1/2}\end{eqnarray}$$

as the reference length scale, and $N_{0}L_{0}=(B_{0}/N_{0})^{1/2}$ as the reference velocity scale. (Henceforth, the symbol $\equiv$ indicates a definition.) The characteristic length scale $L_{0}$ will be referred to as the reference Ozmidov length. This scale provides a reference value of the Ozmidov length

(2.5) $$\begin{eqnarray}L_{Oz}\equiv \left(\frac{\unicode[STIX]{x1D700}}{N^{3}}\right)^{1/2}\end{eqnarray}$$

in the entrainment zone, since the viscous dissipation rate $\unicode[STIX]{x1D700}$ in shear-free CBLs is an order-of-one fraction of the surface buoyancy flux $B_{0}$ (Fedorovich, Conzemius & Mironov Reference Fedorovich, Conzemius and Mironov2004b ), and the mean buoyancy gradient $N^{2}$ is partly characterized by $N_{0}^{2}$ (Garcia & Mellado Reference Garcia and Mellado2014). The Ozmidov length represents the size of the largest motions unaffected by a background stratification $N^{2}$ in a turbulent field characterized by a viscous dissipation rate  $\unicode[STIX]{x1D700}$ (Dougherty Reference Dougherty1961; Ozmidov Reference Ozmidov1965). Garcia & Mellado (Reference Garcia and Mellado2014) and Mellado, Puche & van Heerwaarden (Reference Mellado, Puche and van Heerwaarden2017) have shown that, in shear-free CBLs, $L_{0}$ helps characterize the main properties in the upper region of the entrainment zone, such as the mean gradients and variances of temperature and specific humidity. We will show that $L_{0}$ is also a useful parameter to characterize the entrainment zone in the sheared CBLs considered in this study.

The shear-free limit is fully characterized by a reference buoyancy Reynolds number

(2.6) $$\begin{eqnarray}Re_{0}\equiv \frac{(N_{0}L_{0})L_{0}}{\unicode[STIX]{x1D708}}=\frac{B_{0}}{\unicode[STIX]{x1D708}N_{0}^{2}}\end{eqnarray}$$

and the Prandtl number $Pr\equiv \unicode[STIX]{x1D708}/\unicode[STIX]{x1D705}_{b}$ . The parameter $Re_{0}$ provides a reference value of the buoyancy Reynolds number

(2.7) $$\begin{eqnarray}Re_{b}\equiv \frac{\unicode[STIX]{x1D700}}{\unicode[STIX]{x1D708}N^{2}}\end{eqnarray}$$

in the lower part of the entrainment zone, since $\unicode[STIX]{x1D700}\sim B_{0}$ and $N\sim N_{0}$ in shear-free CBLs, as explained before. A buoyancy Reynolds number is often used in the study of the interaction between turbulence and stable stratification (see e.g. Smyth & Moum Reference Smyth and Moum2000a ; Hebert & de Bruyn Kops Reference Hebert and de Bruyn Kops2006; Chung & Matheou Reference Chung and Matheou2012; Portwood et al. Reference Portwood, de Bruyn Kops, Taylor, Salehipour and Caulfield2016). As explained in the introduction, the work presented here helps ascertain to what extent results from those previous studies apply to the entrainment zone of sheared CBLs.

To characterize wind-shear effects, we use the reference Froude number

(2.8) $$\begin{eqnarray}Fr_{0}\equiv \frac{U_{0}}{N_{0}L_{0}}=\frac{U_{0}}{(B_{0}L_{0})^{1/3}}\end{eqnarray}$$

as the third non-dimensional parameter. The denominator is the velocity scale that stems from the buoyancy acceleration $N_{0}^{2}L_{0}$ associated with a vertical displacement $L_{0}$ in an environment with a buoyancy stratification $N_{0}^{2}$ . The last equality follows from the definition of $L_{0}$ and indicates that $Fr_{0}$ can be interpreted as the ratio between the wind velocity in the free atmosphere and the velocity scale associated with motions of size $L_{0}$ in a turbulent cascade characterized by an energy transfer rate  $B_{0}$ , as is the case in shear-free CBLs.

Owing to statistical homogeneity in the horizontal directions, statistical properties are only functions of two independent variables, namely, height and time $\{z,t\}$ . Following previous work in shear-free CBLs growing into linearly stratified atmospheres (Garcia & Mellado Reference Garcia and Mellado2014; van Heerwaarden & Mellado Reference van Heerwaarden and Mellado2016; Mellado et al. Reference Mellado, van Heerwaarden and Garcia2016), we use the non-dimensionalized form of these variables $\{z/z_{enc},z_{enc}/L_{0}\}$ . The variable $z_{enc}$ is the encroachment length scale defined as

(2.9) $$\begin{eqnarray}z_{enc}\equiv \left\{2N_{0}^{-2}\int _{0}^{z_{\infty }}[\langle b\rangle (z,t)-N_{0}^{2}z]\,\text{d}z\right\}^{1/2},\end{eqnarray}$$

where $z_{\infty }$ is located far enough into the non-turbulent free atmosphere for the integral to become approximately independent of $z_{\infty }$ . Angle brackets denote averaging along horizontal planes. The integral analysis of the buoyancy equation (2.1c ) yields

(2.10) $$\begin{eqnarray}\frac{z_{enc}}{L_{0}}=[2(1+Re_{0}^{-1})N_{0}(t-t_{0})]^{1/2},\end{eqnarray}$$

where $t_{0}$ is a constant of integration, so that $z_{enc}$ can be easily calculated at any time. The reason to use $z_{enc}$ instead of time as independent variable is that the encroachment length scale provides a measure of the shear-free CBL depth (Carson & Smith Reference Carson and Smith1975), and it can be calculated from the mean buoyancy profile according to (2.9), which makes it convenient for the interpretation of results. We will show that $z_{enc}$ also provides a relevant depth measure for the sheared CBLs considered in this study.

The sheared CBL can also be partly characterized by the stability parameter defined as the ratio between the CBL depth and the Obukhov length (Stull Reference Stull and Stull1988). The Obukhov length is defined as

(2.11) $$\begin{eqnarray}L_{Ob}\equiv -\frac{u_{\ast }^{3}}{\unicode[STIX]{x1D705}B_{0}}=-\left(\frac{u_{\ast }}{w_{\ast }}\right)^{3}\frac{z_{enc}}{\unicode[STIX]{x1D705}},\end{eqnarray}$$

where $\unicode[STIX]{x1D705}\simeq 0.41$ is the von Kármán constant,

(2.12) $$\begin{eqnarray}u_{\ast }\equiv (\unicode[STIX]{x1D708}\unicode[STIX]{x2202}_{z}\langle u\rangle )_{z=0}^{1/2}\end{eqnarray}$$

is the friction velocity and

(2.13) $$\begin{eqnarray}w_{\ast }\equiv (B_{0}z_{enc})^{1/3}\end{eqnarray}$$

is a convective velocity scale (Deardorff Reference Deardorff1970). Very large values of $-z_{enc}/L_{Ob}$ correspond to nearly shear-free CBLs, and very small values correspond to nearly neutral, shear-driven boundary layers. When studying entrainment-zone properties, however, the stability parameter alone is not sufficient as an independent variable, and alternative options have been proposed, such as a Richardson number (see Conzemius & Fedorovich Reference Conzemius and Fedorovich2006b ; Pino & Vilà-Guerau De Arellano Reference Pino and Vilà-Guerau De Arellano2008; and references therein). We will discuss these alternative variables in § 6.

2.3 Parameter space and description of simulations

For typical midday conditions, $N_{0}\simeq (0.6{-}1.8)\times 10^{-2}~\text{s}^{-1}$ , $B_{0}\simeq (0.3{-}1.0)\times 10^{-2}~\text{m}^{2}~\text{s}^{-3}$ and $z_{enc}\simeq 500{-}2000~\text{m}$ , one finds $L_{0}\simeq 20{-}200~\text{m}$ and states of development in the range $z_{enc}/L_{0}\simeq 5{-}50$ . For these conditions and wind velocities in the interval $U_{0}=0{-}15~\text{m}~\text{s}^{-1}$ , the reference Froude number is in the range $Fr_{0}\simeq 0{-}35$ . Using $\unicode[STIX]{x1D705}_{b}=2.1\times 10^{-5}~\text{m}^{2}~\text{s}^{-1}$ and $\unicode[STIX]{x1D708}=1.5\times 10^{-5}~\text{m}^{2}~\text{s}^{-1}$ , one further obtains $Re_{0}\simeq 6\times 10^{5}$ to $2\times 10^{7}$ and $Pr\simeq 0.7$ .

Table 1.

Simulation properties. Columns 3–8 provide data at the final time of the simulations, and columns 9–11 show the variation between $z_{enc}/L_{0}=15$ and the final time of the simulations. Here $Re_{0}$ is the reference buoyancy Reynolds number defined by (2.6);  $Fr_{0}$ is the reference Froude number defined by (2.8);  $z_{enc}$ is the encroachment length defined by (2.9); and $L_{0}$ is the reference Ozmidov length defined by (2.4). The convective Reynolds number is defined as $Re_{\ast }\equiv z_{enc}w_{\ast }/\unicode[STIX]{x1D708}$ , where $w_{\ast }$ is the convective velocity scale defined by (2.13). The turbulent Reynolds number is defined as $Re_{t}\equiv e^{2}/\unicode[STIX]{x1D700}\unicode[STIX]{x1D708}$ , where $e$ is the TKE and $\unicode[STIX]{x1D700}$ its viscous dissipation rate; $(Re_{t})_{max}$ is the maximum turbulent Reynolds number in the CBL; and $(Re_{t})_{z_{i,f}}$ is the turbulent Reynolds number particularized at the height of the minimum buoyancy flux. $(Re_{b})_{z_{i,f}}$ is the buoyancy Reynolds number defined by (2.7) particularized at the height of the minimum buoyancy flux; $\unicode[STIX]{x1D702}\equiv (\unicode[STIX]{x1D708}^{3}/\unicode[STIX]{x1D700})^{1/4}$ is the Kolmogorov scale; $(\unicode[STIX]{x0394}z_{i})_{c}$ and $(\unicode[STIX]{x0394}z_{i})_{s}$ are defined by (4.9) and (4.10), respectively, and are the convective and shear limits of the entrainment-zone scale, which is defined by (4.6);  $L_{Ob}$ is the Obukhov length defined by (2.11).

In our simulations, we fix $Pr=1$ and change the reference Froude number between zero (no wind condition) and 25 (strong wind condition) in intervals of 5. Table 1 summarizes the configurations studied in this work. We reach $z_{enc}/L_{0}\simeq 35$ , covering in this way a large extent of the typical values observed in nature. The stability parameter $-z_{enc}/L_{Ob}$ is larger than 4. Hence, we cover the regime of weakly unstable conditions $0<-z_{enc}/L_{Ob}\lesssim 15{-}20$ , characterized by horizontal convective rolls aligned with the mean wind direction, as well as the regime of strongly unstable conditions, characterized by polygonal convective cells (LeMone Reference Lemone1973; Moeng & Sullivan Reference Moeng and Sullivan1994; Salesky et al. Reference Salesky, Chamecki and Bou-Zeid2017). The reference Reynolds number that we achieve in our simulations, however, is much smaller than in the atmosphere. Nonetheless, the entrainment zone is largely occupied with turbulent patches, as shown in figure 2. We use data from simulations with $Re_{0}=25$ , $Re_{0}=42$ and $Re_{0}=117$ . The main analysis is based on the simulations with $Re_{0}=25$ because these cases reach higher values of state of development $z_{enc}/L_{0}$ , and, unless otherwise stated, the figures show data from these simulations. The cases with $Re_{0}=42$ are used to study the sensitivity of the results to the Reynolds number; for the shear-free cases, we also compare to case $Re_{0}=117$ . Although this range of Reynolds number is small, the observed tendency towards Reynolds-number similarity is consistent with that observed in previous work in similar configurations, and supports the use of DNS to study some aspects of the atmospheric boundary layer (Jonker et al. Reference Jonker, van Reeuwijk, Sullivan and Patton2013; Waggy, Biringen & Sullivan Reference Waggy, Biringen and Sullivan2013; Garcia & Mellado Reference Garcia and Mellado2014; van Heerwaarden & Mellado Reference van Heerwaarden and Mellado2016; Mellado et al. Reference Mellado, Bretherton, Stevens and Wyant2018).

Figure 2.

Horizontal cross-section of the standardized natural logarithm of the viscous dissipation rate $\unicode[STIX]{x1D716}\equiv \unicode[STIX]{x1D708}(\unicode[STIX]{x2202}_{i}u_{j}^{\prime }+\unicode[STIX]{x2202}_{j}u_{i}^{\prime })\unicode[STIX]{x2202}_{j}u_{i}^{\prime }$ at the height of the minimum buoyancy flux from case $Fr_{0}=20$ and $Re_{0}=42$ of table 1 at $z_{enc}/L_{0}\simeq 15$ . Primes indicate turbulent-fluctuation fields.

The domain size is $215L_{0}\times 215L_{0}\times 130L_{0}$ in all cases, and stopping the simulation at $z_{enc}/L_{0}\simeq 35$ implies that the boundary layer occupies approximately $30\,\%$ of the computational domain. Preliminary studies have shown that this ratio between the CBL depth and the depth of the computational domain is small enough for results to be independent of the depth of the computational domain. The aspect ratio of the horizontal domain size and the CBL depth varies between $12:1$ at the beginning of the quasi-steady regime to around $5:1$ at the final time considered in the analysis. The thickness $\unicode[STIX]{x1D6FF}_{0}$ used in the initial conditions (2.2) and (2.3) is $\unicode[STIX]{x1D6FF}_{0}\simeq 0.2L_{0}$ , small compared to $z_{enc}\simeq 10L_{0}$ , which is when the quasi-steady regime in shear-free CBLs starts. Preliminary studies considering additional perturbations in the velocity field over a similarly thin region have shown that results are independent of the details of the initial conditions.

Table 2.

Grid resolution. Here $\unicode[STIX]{x1D6E5}_{x}$ , $\unicode[STIX]{x1D6E5}_{y}$ and $\unicode[STIX]{x1D6E5}_{z}$ are the grid spacings in the streamwise, spanwise and vertical directions, respectively. The maximum value of $\unicode[STIX]{x1D6E5}_{z}/\unicode[STIX]{x1D702}$ occurs at the final time of the simulations, while the maximum values of $\unicode[STIX]{x1D6E5}_{x}^{+}$ , $\unicode[STIX]{x1D6E5}_{y}^{+}$ and $\unicode[STIX]{x1D6E5}_{z}^{+}$ take place at the very beginning of the simulations, when the friction velocity is large. The last column shows the variation between $z_{enc}/L_{0}=15$ and the final time of the simulations.

Apart from the case $Fr_{0}=20$ , the grid spacings are uniform and isotropic in all of the computational domain except near the surface and in the free atmosphere above the turbulent boundary layer (see table 2). As we move towards the surface, the vertical grid spacing is smoothly refined according to a hyperbolic tangent profile to provide the required higher resolution near the surface. The ratio between the vertical grid spacing in the bulk of the CBL and near the surface is 2.5, which is roughly the ratio between the Kolmogorov length scale in the bulk of the turbulent layer and near the surface in convection-dominated flows (Shishkina et al. Reference Shishkina, Stevens, Grossmann and Lohse2010; Mellado Reference Mellado2012). The grid stretching associated with this refinement concentrates between $z=3L_{0}$ and $z=15L_{0}$ and the stretching factor is less than 1.5 %, which has been shown to be small enough to maintain the high accuracy of the compact schemes used in this work (Mellado & Ansorge Reference Mellado and Ansorge2012). As we move upwards outside of the turbulent boundary layer and into the non-turbulent free atmosphere, the vertical grid spacing is smoothly coarsened according to a second hyperbolic tangent profile. The aim is to extend the vertical size of the computational domain and reduce the effect of the spurious reflection of gravity waves at the top of the computational domain without an excessive penalty in the required number of grid points. This coarsening starts beyond $z=55L_{0}$ , which is well above the turbulent boundary layer, and the corresponding stretching factor is less than 3.5 %. We used preliminary studies to ascertain that the results were insensitive to the details of the grid.

The grid spacings are chosen according to the well-established resolution requirements for shear-driven flows (Flores, Jiménez & Del Álamo Reference Flores, Jiménez and Del Álamo2007; Spalart, Coleman & Johnstone Reference Spalart, Coleman and Johnstone2008; Bernardini, Pirozzoli & Orlandi Reference Bernardini, Pirozzoli and Orlandi2014) and convection-driven flows (Shishkina et al. Reference Shishkina, Stevens, Grossmann and Lohse2010; Mellado Reference Mellado2012; Waggy et al. Reference Waggy, Biringen and Sullivan2013). The vertical grid spacing,  $\unicode[STIX]{x1D6E5}_{z}$ , always satisfies the relation $\unicode[STIX]{x1D6E5}_{z}/\unicode[STIX]{x1D702}\lesssim 1.5$ (cf. table 2), where $\unicode[STIX]{x1D702}\equiv (\unicode[STIX]{x1D708}^{3}/\unicode[STIX]{x1D700})^{1/4}$ is the Kolmogorov scale. This ratio is sufficient for the statistical properties of interest to depend less than $5\,\%$ on the grid spacing, which is comparable to or less than the statistical convergence of the properties considered in the present work (Mellado Reference Mellado2012; Garcia & Mellado Reference Garcia and Mellado2014). We also keep $\unicode[STIX]{x1D6E5}_{x}^{+}=\unicode[STIX]{x1D6E5}_{y}^{+}\lesssim 4.5$ , where superscript $+$ denotes quantities normalized with the wall unit $\unicode[STIX]{x1D708}/u_{\ast }$ (Ansorge & Mellado Reference Ansorge and Mellado2014; Gohari & Sarkar Reference Gohari and Sarkar2017; Pirozzoli et al. Reference Pirozzoli, Bernardini, Verzicco and Orlandi2017). Moreover, the viscous sublayer is resolved by $\simeq 10$ grid points in all simulations (Spalart et al. Reference Spalart, Coleman and Johnstone2008; Gohari & Sarkar Reference Gohari and Sarkar2017). The reason for the anisotropic grid in the horizontal directions in the cases with $Fr_{0}=20$ is that we could satisfy the aforementioned resolution constraints without the need to reduce the grid spacing in the streamwise direction with respect to the corresponding cases with $Fr_{0}=15$ , which allowed us to save computational time.

To improve statistical convergence and thus the clarity of the results discussed below, horizontal averages are additionally averaged in time over an interval $\unicode[STIX]{x0394}z_{enc}/L_{0}=2$ , which means $\simeq 6$ large-eddy turnover times at $z_{enc}/L_{0}=30$ . This time interval is small compared to the time required for the mean properties to change significantly. When plotting the data, lines indicate this running average within an interval $\unicode[STIX]{x0394}z_{enc}/L_{0}=2$ , and shadow regions indicate the interval of two standard deviations around that average.

2.4 Equilibrium (quasi-steady) entrainment regime

Garcia & Mellado (Reference Garcia and Mellado2014) have shown that the equilibrium (quasi-steady) entrainment regime is reached beyond $z_{enc}/L_{0}\simeq 10$ in shear-free CBLs growing into linearly stratified atmospheres. In order to evaluate if the wind shear changes this critical value, following Fedorovich et al. (Reference Fedorovich, Conzemius and Mironov2004b ), we perform an integral analysis of the TKE evolution equation

(2.14) $$\begin{eqnarray}\unicode[STIX]{x2202}_{t}e=P+\langle b^{\prime }w^{\prime }\rangle -\unicode[STIX]{x2202}_{z}T-\unicode[STIX]{x1D700},\end{eqnarray}$$

where $\unicode[STIX]{x2202}_{t}e$ is the accumulation term, $P\equiv -\langle u^{\prime }w^{\prime }\rangle \unicode[STIX]{x2202}_{z}\langle u\rangle$ is the shear-production rate, $\langle b^{\prime }w^{\prime }\rangle$ is the buoyancy production or destruction rate, $-\unicode[STIX]{x2202}_{z}T$ is the turbulent transport, where $T\equiv \langle u_{i}^{\prime }u_{i}^{\prime }w^{\prime }/2+p^{\prime }w^{\prime }-u_{i}^{\prime }\unicode[STIX]{x1D70F}_{i3}^{\prime }\rangle$ , and $\unicode[STIX]{x1D700}\equiv \langle \unicode[STIX]{x1D70F}_{ij}^{\prime }\unicode[STIX]{x2202}_{j}u_{i}^{\prime }\rangle$ is the viscous dissipation rate, $\unicode[STIX]{x1D70F}_{ij}\equiv \unicode[STIX]{x1D708}(\unicode[STIX]{x2202}_{i}u_{j}+\unicode[STIX]{x2202}_{j}u_{i})$ being the kinematic components of the viscous stress tensor. Primes indicate turbulent-fluctuation fields, e.g. $b^{\prime }\equiv b-\langle b\rangle$ . Integrating (2.14) from the surface to a height $z_{\infty }$ far into the non-turbulent free atmosphere yields

(2.15) $$\begin{eqnarray}\int _{0}^{z_{\infty }}\unicode[STIX]{x2202}_{t}e\,\text{d}z=\int _{0}^{z_{\infty }}(P+\langle b^{\prime }w^{\prime }\rangle -\unicode[STIX]{x2202}_{z}T-\unicode[STIX]{x1D700})\,\text{d}z,\end{eqnarray}$$

which for simplicity we write as

(2.16) $$\begin{eqnarray}I_{t}=I_{P}+I_{bw}+I_{T}-I_{\unicode[STIX]{x1D700}}.\end{eqnarray}$$

The temporal evolution of each term normalized by $w_{\ast }^{3}$ is shown in figure 3. (Curves in this figure correspond to the upper limit of integration $z_{\infty }=2.5z_{enc}$ , but results remain similar when varying this limit between $1.5z_{enc}$ and $2.5z_{enc}$ .) Similar to the shear-free case, the normalized integral of the transport term $I_{T}$ is small, which implies that the energy drain due to the upward radiation of gravity waves is negligible. Moreover, the normalized integral of the temporal term $I_{t}$ becomes negligible beyond $z_{enc}/L_{0}\simeq 10$ –15, implying that there is a balance between shear production, buoyancy production and viscous dissipation, i.e. $I_{bw}+I_{P}\simeq I_{\unicode[STIX]{x1D700}}$ . This balance corresponds to the equilibrium (quasi-steady) entrainment regime. In this work, we focus on this regime and study wind-shear effects beyond $z_{enc}/L_{0}\simeq 15$ , and we will only consider the data in the quasi-steady regime to derive scaling laws. However, we will plot the data starting at $z_{enc}/L_{0}=5$ to indicate how the statistics approach the quasi-steady regime.

Figure 3.

Temporal evolution of the terms of the integral TKE budget equation (2.16) normalized with the convective velocity scale, defined in (2.13). Lines indicate the average within an interval $\unicode[STIX]{x0394}z_{enc}/L_{0}=2$ , and shadow regions indicate the interval of two standard deviations around that average.

3.1 Effects on the buoyancy

Figure 4.

Vertical profiles of (a) the mean buoyancy normalized by the encroachment buoyancy, defined by (3.1), and (b) the buoyancy flux, defined by (3.2), normalized by the surface buoyancy flux, for different Froude numbers at $z_{enc}/L_{0}\simeq 30$ . Data have been averaged within an interval $\unicode[STIX]{x0394}z_{enc}/L_{0}=2$ .

In the mixed layer, i.e. the well-mixed region between $z\simeq 0.1z_{enc}$ and $z\simeq z_{enc}$ , the mean buoyancy increases in time due to the surface buoyancy flux and the entrainment flux. In our study, the surface flux is constant and independent of the wind velocity, but the entrainment flux increases with the wind velocity, and therefore the mean buoyancy in the mixed layer is expected to increase with $Fr_{0}$ . Previous studies have shown, however, that this increase is weak (e.g. Kim et al. Reference Kim, Park and Moeng2003; Pino, Vilà-Guerau De Arellano & Duynkerke Reference Pino, Vilà-Guerau De Arellano and Duynkerke2003; Pino & Vilà-Guerau De Arellano Reference Pino and Vilà-Guerau De Arellano2008), so that the encroachment buoyancy (Carson & Smith Reference Carson and Smith1975)

(3.1) $$\begin{eqnarray}b_{enc}\equiv N_{0}^{2}z_{enc}\end{eqnarray}$$

characterizes the mean buoyancy in the mixed layer not only in shear-free conditions but also in sheared CBLs under weakly to strongly unstable conditions. Figure 4(a) confirms this result up to wind velocities corresponding to $Fr_{0}=25$ , for which the mean buoyancy is only $\simeq 2$  % higher than in shear-free conditions. Wind-shear effects on the buoyancy flux

(3.2) $$\begin{eqnarray}B\equiv \langle b^{\prime }w^{\prime }\rangle -\unicode[STIX]{x1D705}_{b}\unicode[STIX]{x2202}_{z}\langle b\rangle\end{eqnarray}$$

are also negligible in the mixed layer for all Froude numbers considered in this study (figure 4 b). In contrast, in the entrainment zone, the region of negative buoyancy flux above the mixed layer, wind-shear effects become significant for Froude numbers larger than 10. Hence, in agreement with the aforementioned previous studies where Coriolis effects are retained, wind-shear effects on buoyancy properties remain localized inside the entrainment zone for the idealized CBLs considered in this study.

To better quantify the effect of the wind shear on entrainment-zone properties, we plot the temporal evolution of the minimum buoyancy flux normalized by the surface buoyancy flux, $-B_{z_{i,f}}/B_{0}$ , in figure 5(a). (Henceforth, the subscript $z_{i,\unicode[STIX]{x1D709}}$ indicates that the corresponding quantity is evaluated at $z_{i,\unicode[STIX]{x1D709}}$ , and $z_{i,f}$ is the height of the minimum buoyancy flux.) For $Fr_{0}\lesssim 10$ , this quantity approximately coincides with that of the shear-free case for $z_{enc}/L_{0}\gtrsim 10{-}15$ , which indicates a negligible effect of wind shear on the minimum buoyancy flux during the quasi-steady regime. The slight decrease for weak shear conditions $Fr_{0}=5$ at early states of development $z_{enc}/L_{0}\lesssim 15$ has also been observed in Pino & Vilà-Guerau De Arellano (Reference Pino and Vilà-Guerau De Arellano2008), and it might be a manifestation of the sheltering effect of shear on the propagation of turbulence near a turbulent/non-turbulent interface (Hunt & Durbin Reference Hunt and Durbin1999; Fedorovich & Thäter Reference Fedorovich and Thäter2001), or of the enhancement of the energy drain from the CBL top by gravity-wave radiation into the free atmosphere (Schröter Reference Schröter2018). However, more analysis would be required to draw a definitive conclusion because the effect of the shear near the surface might still be significant in such a shallow CBL. For Froude numbers larger than 10, the ratio $-B_{z_{i,f}}/B_{0}$ increases. Visualizations show that Kelvin–Helmholtz-like instabilities inside the entrainment zone are associated with this increase (cf. figure 1), in agreement with previous observations (Kim et al. Reference Kim, Park and Moeng2003).

Figure 5.

Temporal evolution of (a) the minimum buoyancy flux normalized by the surface buoyancy flux, and (b) different definitions of the CBL depth normalized by the encroachment length scale. For clarity, in panel (b), the height of the maximum buoyancy gradient, $z_{i,g}$ , is indicated by dashed lines.

Another property that proves useful for the analysis of wind-shear effects on entrainment-zone properties is the CBL depth. We consider the following definitions of the CBL depth (see e.g. Garratt Reference Garratt1992; Sullivan et al. Reference Sullivan, Moeng, Stevens, Lenschow and Mayor1998): (i) the zero-crossing height, $z_{i,0}$ , where the buoyancy flux becomes zero; (ii) the flux-based height, $z_{i,f}$ , where the buoyancy flux is minimum; and (iii) the gradient-based height, $z_{i,g}$ , where the mean buoyancy gradient is maximum. The temporal evolution of these heights, shown in figure 5(b), corroborates the features discussed before. First, the zero-crossing height $z_{i,0}$ , which marks the bottom of the entrainment zone, is independent of the wind strength and it is well approximated by the encroachment length scale, $z_{enc}$ . This result further indicates that wind-shear effects above the surface layer on the mean buoyancy concentrate in the entrainment zone (Fedorovich & Conzemius Reference Fedorovich and Conzemius2008; Pino & Vilà-Guerau De Arellano Reference Pino and Vilà-Guerau De Arellano2008). Second, the difference in $z_{i,f}$ and $z_{i,g}$ between cases $Fr_{0}=0$ and $Fr_{0}=10$ is small, which further indicates that entrainment-zone properties remain unchanged for such a weak wind condition. Third, for stronger wind conditions, wind-shear effects in the entrainment zone become considerable, and both $z_{i,f}$ and $z_{i,g}$ increase. We note that, although the change of these heights is small relative to the CBL depth, those changes are approximately 100 % of the entrainment-zone thickness, and are relevant for the local analysis of the entrainment zone in § 4.

Figure 5(a,b) also shows that wind-shear effects diminish and eventually vanish as the CBL grows and thermals ascending from the mixed layer become more vigorous and dominate mixing in the entrainment zone (Mahrt & Lenschow Reference Mahrt and Lenschow1976; Pino & Vilà-Guerau De Arellano Reference Pino and Vilà-Guerau De Arellano2008; Liu, Sun & Shen Reference Liu, Sun and Shen2016). Hence, shear effects depend not only on the Froude number $Fr_{0}$ , or, equivalently, the wind velocity in the free atmosphere, but also on the normalized CBL depth $z_{enc}/L_{0}$ . In § 5, we find a non-dimensional variable that embeds the dependence on both $Fr_{0}$ and $z_{enc}/L_{0}$ , which facilitates the characterization of wind-shear effects.

3.2 Effects on the velocity

Figure 6.

Vertical profiles of (a) the mean streamwise velocity normalized by the wind velocity in the free atmosphere, $U_{0}$ , and (b) the momentum flux normalized with $U_{0}$ and the reference convection velocity $N_{0}L_{0}$ . Data correspond to case $Fr_{0}=25$ at different $z_{enc}/L_{0}$ .

As seen in figure 6(a), when the CBL depth becomes an order of magnitude larger than $L_{0}$ , the velocity profile varies rapidly across the CBL top, and becomes almost flat within the mixed layer. Because of this flat shape, the vertically averaged mean velocity

(3.3) $$\begin{eqnarray}u_{ml}\equiv \frac{1}{z_{i,f}}\int _{0}^{z_{i,f}}\langle u\rangle \,\text{d}z\end{eqnarray}$$

provides an appropriate characteristic scale, and velocity profiles normalized by $u_{ml}$ collapse on top of each other and exhibit self-similarity within the mixed layer. This vertical structure consisting of a well-mixed velocity profile in the mixed layer and an elevated wind shear in the entrainment zone is characteristic of the weakly to strongly unstable conditions $-z_{enc}/L_{Ob}\gtrsim 4$ considered in this study (Kim et al. Reference Kim, Park and Moeng2003; Conzemius & Fedorovich Reference Conzemius and Fedorovich2006a ; Sorbjan Reference Sorbjan2006; Pino & Vilà-Guerau De Arellano Reference Pino and Vilà-Guerau De Arellano2008). Hence, the idealized CBL considered in this study also reproduces this main feature of barotropic CBLs in middle latitudes, despite neglecting Coriolis effects.

The corresponding profiles of the kinematic momentum flux

(3.4) $$\begin{eqnarray}\unicode[STIX]{x1D70F}_{x}\equiv \langle u^{\prime }w^{\prime }\rangle -\unicode[STIX]{x1D708}\frac{\unicode[STIX]{x2202}\langle u\rangle }{\unicode[STIX]{x2202}z}\end{eqnarray}$$

are shown in figure 6(b). Horizontal momentum is entrained at the CBL top, transported down across the mixed layer, and finally removed by friction at the surface. The larger magnitude of the momentum flux at the surface compared to the entrainment zone causes the momentum inside the mixed layer to decrease in time (figure 6 a). However, the difference between the momentum flux at the surface and at the CBL top decreases in time, which implies a decrease in the time rate of change of the mean velocity in the mixed layer.

Figure 7.

Vertical profiles of (a) the TKE budget and (b) the r.m.s. of the vertical velocity at $z_{enc}/L_{0}\simeq 30$ . Data from case $Fr_{0}=10$ correspond to the transition from a convection-dominated regime in the entrainment zone to a shear-dominated regime, and data from case $Fr_{0}=25$ correspond to a shear-dominated regime ( $(\unicode[STIX]{x0394}z_{i})_{s}/(\unicode[STIX]{x0394}z_{i})_{c}\approx 0.43$ and $(\unicode[STIX]{x0394}z_{i})_{s}/(\unicode[STIX]{x0394}z_{i})_{c}\approx 1.21$ , respectively; see figure 17 and table 3).

The TKE budget is shown in figure 7(a). For $Fr_{0}=10$ , the strong shear production of TKE near the surface changes the transport and dissipation terms, but those changes remain constrained to a depth below $\simeq 0.25z_{enc}$ : compared to the shear-free case, the turbulent transport additionally removes energy from very near the surface, below $\simeq 0.05z_{enc}$ , and deposits it in a thin layer above that region, between $\simeq 0.05z_{enc}$ and $\simeq 0.25z_{enc}$ . The turbulent transport remains unchanged in the CBL interior, between $\simeq 0.25z_{enc}$ and $\simeq 0.9z_{enc}$ . In the entrainment zone, the reduction of turbulent transport approximately compensates the shear production, while the buoyancy flux and viscous dissipation remain practically the same as in shear-free conditions.

For stronger shear conditions, such as for $Fr_{0}=25$ , the changes near the surface become larger but the turbulent transport still seems to redistribute TKE within a region below $\simeq 0.25z_{enc}$ , which indicates that shear-generated turbulence near the surface is not responsible for the shear enhancement of entrainment (Conzemius & Fedorovich Reference Conzemius and Fedorovich2006a ; Fedorovich & Conzemius Reference Fedorovich and Conzemius2008). In contrast, the changes in the entrainment zone are now more substantial. The turbulent transport develops a local minimum close to zero at the height of maximum shear production, and the magnitudes of the buoyancy flux and dissipation rate increase. We also observe a slight change in the turbulent transport in the CBL interior, a displacement of the curve towards the right. This change indicates that, with respect to the shear-free case, less TKE is being transported from the lower half of the CBL to the upper half, or that shear-generated TKE in the entrainment zone is actually being transported downwards towards the CBL interior. The magnitude of the dissipation rate in the CBL interior increases accordingly.

The variance of the vertical velocity, shown in figure 7(b), further stresses the importance of shear across the entrainment zone compared to the shear near the surface, since the curves for different Froude numbers differ for $z\gtrsim z_{enc}$ but approximately collapse on top of each other for $z\lesssim z_{enc}$ . In this region, the parametrization for $w_{rms}$ proposed by Lenschow, Wyngaard & Pennell (Reference Lenschow, Wyngaard and Pennell1980) provides accurate estimates for the weakly to strongly unstable conditions $-z_{enc}/L_{Ob}\gtrsim 4$ considered here.

4.1 The two-layer structure of the entrainment zone in the shear-free CBL

The analysis presented in this section is based on previous work on shear-free CBLs by Garcia & Mellado (Reference Garcia and Mellado2014), who described the entrainment zone as a composition of two sublayers (cf. figure 9). The lower entrainment-zone (EZ) sublayer is located around $z_{i,f}$ and is characterized by a length scale proportional to the CBL depth and by the convective scales derived from the CBL depth and the surface buoyancy flux (Deardorff Reference Deardorff1970). The scaling law for $z_{i,f}$ in shear-free CBLs is (figure 10 a)

(4.2) $$\begin{eqnarray}z_{i,f}-z_{enc}\simeq 0.14z_{enc}.\end{eqnarray}$$

On the left-hand side, we measure distances with respect to $z_{enc}$ , the encroachment length scale, because $z_{enc}$ provides an analytical reference height for the position of the entrainment zone, and subtracting this order-of-one quantity allows us to emphasize the local structure. (By ‘scaling law’ we mean functional relationships between dependent and independent variables that are consistent with the dimensional analysis presented in § 2.2.)

Figure 9.

Sketch of the vertical structure of the CBL-top region. Here $z_{i,0}$ is the zero-crossing height; $z_{i,f}$ is the height of the minimum buoyancy flux; $z_{i,s}$ marks the transition from the lower EZ sublayer to the upper EZ sublayer; and $z_{i,g}$ is the height of the maximum buoyancy gradient. Red indicates the upper EZ sublayer, yellow indicates the lower EZ sublayer, and blue indicates the mixed layer.

The upper EZ sublayer is centred around $z_{i,g}$ , acts as a transition layer between the turbulent region below and the non-turbulent stably stratified region above, and is characterized by local scales. The local length scale is $(L_{Oz})_{z_{i,f}}$ , the Ozmidov scale defined in (2.5) particularized at the height of the minimum buoyancy flux $z_{i,f}$ . Since the upper EZ sublayer, which is characterized by $(L_{Oz})_{z_{i,f}}$ , is on top of the lower EZ sublayer, which is characterized by $z_{enc}$ , we seek a scaling law for $z_{i,g}$ of the form

(4.3) $$\begin{eqnarray}z_{i,g}-z_{enc}\simeq \unicode[STIX]{x1D6FC}_{c}z_{enc}+\unicode[STIX]{x1D6FD}_{c}(L_{Oz})_{z_{i,f}},\end{eqnarray}$$

where $\unicode[STIX]{x1D6FC}_{c}$ and $\unicode[STIX]{x1D6FD}_{c}$ are constants to be determined. This ansatz is supported by figure 10(b). A linear regression to the data for $z_{enc}/L_{0}\gtrsim 15$ provides the values $\unicode[STIX]{x1D6FC}_{c}=0.184$ and $\unicode[STIX]{x1D6FD}_{c}=1.78$ . Equation (4.3) extends the result $z_{i,g}\propto z_{enc}$ proposed in Garcia & Mellado (Reference Garcia and Mellado2014) with a first-order correction proportional to $(L_{Oz})_{z_{i,f}}$ .

We can define

(4.4) $$\begin{eqnarray}z_{i,s}\equiv z_{i,g}-\unicode[STIX]{x1D6FD}_{c}(L_{Oz})_{z_{i,f}}\end{eqnarray}$$

as a reference height that marks the transition from the lower EZ sublayer to the upper EZ sublayer, i.e. the transition from a region characterized by $z_{enc}$ to a region characterized by $(L_{Oz})_{z_{i,f}}$ . The upper boundary of the entrainment zone, and thus the upper boundary of the CBL, can be estimated as $z_{i,g}+1.78(L_{Oz})_{z_{i,f}}$ . The thickness of the upper EZ sublayer can be estimated as $2(z_{i,g}-z_{i,s})\simeq 3.56(L_{Oz})_{z_{i,f}}$ . As later discussed in § 5, the length scale $(L_{Oz})_{z_{i,f}}$ varies only weakly in time and it is well approximated by $0.45L_{0}$ , where $L_{0}$ is the reference Ozmidov length.

Figure 10.

Scaling of the flux-based and gradient-based CBL depths in the shear-free CBL in terms of the encroachment length, $z_{enc}$ , and the Ozmidov length $(L_{Oz})_{z_{i,f}}$ . Symbols indicate the average within an interval $\unicode[STIX]{x0394}z_{enc}/L_{0}=2$ . In panel (b), only data for $z_{enc}/L_{0}\gtrsim 15$ are considered.

4.2 The two-layer structure of the entrainment zone in the sheared CBL

How does the two-layer structure of the entrainment zone change with wind in the free atmosphere? As observed in § 3, wind in the free atmosphere leads to the formation of a shear layer in the entrainment zone, i.e. a layer of marked variation of the mean velocity between two regions with homogeneous velocity. From the various idealized configurations often employed to study stably stratified sheared turbulence, the stably stratified shear layer seems appropriate to introduce the discussion on the interaction between shear and stratification in the entrainment zone of the CBL, given the coincidence of a localized shear layer with a localized stratified layer (see e.g. Sherman, Imberger & Corcos Reference Sherman, Imberger and Corcos1978; Peltier & Caulfield Reference Peltier and Caulfield2003; Mashayek & Peltier Reference Mashayek and Peltier2011). The minimum gradient Richardson number

(4.5) $$\begin{eqnarray}Ri_{g}\equiv \frac{\unicode[STIX]{x2202}_{z}\langle b\rangle }{(\unicode[STIX]{x2202}_{z}\langle u\rangle )^{2}}\end{eqnarray}$$

is a major variable characterizing the evolution of stably stratified shear layers. If the initial shear layer is thin enough for the Richardson number to be relatively small, Kelvin–Helmholtz-like instabilities will cause an overturning of the stably stratified fluid and a thickening of the shear layer. As the shear layer thickens, overturning the fluid becomes more difficult because the vertical displacement increases whereas the available kinetic energy, proportional to the squared velocity jump across the shear layer, remains constant. Once the shear layer reaches a critical thickness, or equivalently a critical Richardson number, the available kinetic energy is insufficient to overturn the fluid and turbulence decays. Results show that this critical Richardson number is $1/3\pm 15\,\%$ , the uncertainty interval representing statistical convergence and the dependence on Prandtl number, Reynolds number and initial conditions given that the flow is strongly transient (see e.g. Smyth & Moum Reference Smyth and Moum2000b ; Brucker & Sarkar Reference Brucker and Sarkar2007; Howland, Taylor & Caulfield Reference Howland, Taylor and Caulfield2018).

Figure 11.

Temporal evolution of (a) the gradient Richardson number (4.5), and (b) the normalized buoyancy gradient, both evaluated at the height of the minimum buoyancy flux. Grey area indicates the interval where both shear and convection are important, as discussed in § 6.

In the CBL, convection in the mixed layer underneath the entrainment zone is expected to introduce important differences with respect to the stably stratified shear layer. One difference is that turbulence is sustained for a gradient Richardson number significantly larger than $1/3$ . This is shown in figure 11(a), which plots $Ri_{g}$ at the height of the minimum buoyancy flux, which approximately coincides with the height of the minimum $Ri_{g}$ . The main reason is that convective motions in the CBL make the shear layer locally thinner, which leads to local subcritical Richardson numbers and hence local shear instabilities that maintain a turbulent state (Mahrt & Lenschow Reference Mahrt and Lenschow1976; Kim et al. Reference Kim, Park and Moeng2003; Conzemius & Fedorovich Reference Conzemius and Fedorovich2007). It is curious that the gradient Richardson number in the entrainment zone approaches the value $1/3$ as shear increases, which is the upper value observed in stably stratified shear layers, although there is a priori no strong argument to expect this agreement given the strong differences between the two cases.

To quantify how wind shear modifies the lower EZ sublayer, specifically, the scaling law (4.2) for $z_{i,f}$ , we introduce the length scale

(4.6) $$\begin{eqnarray}\unicode[STIX]{x0394}z_{i}\equiv \frac{\unicode[STIX]{x0394}u}{(\unicode[STIX]{x2202}_{z}\langle u\rangle )_{z_{i,f}}},\end{eqnarray}$$

where

(4.7) $$\begin{eqnarray}\unicode[STIX]{x0394}u\equiv U_{0}-u_{ml}\end{eqnarray}$$

is the velocity difference across the entrainment zone, the mixed-layer value $u_{ml}$ being defined by (3.3). The length scale $\unicode[STIX]{x0394}z_{i}$ is referred to as the vorticity thickness in the literature of stably stratified shear layers. In this work we will refer to $\unicode[STIX]{x0394}z_{i}$ as the EZ scale, because, as shown in the remainder of this section and in § 5, $\unicode[STIX]{x0394}z_{i}$ characterizes the lower EZ sublayer (cf. figure 9). Since the lower EZ sublayer is on top of the mixed layer, which is characterized by $z_{enc}$ , we seek a scaling law for $z_{i,f}$ that is a linear combination of $\unicode[STIX]{x0394}z_{i}$ and $z_{enc}$ . Figure 12(a) supports this ansatz, and a linear regression to the data for $z_{enc}/L_{0}\gtrsim 15$ yields

(4.8) $$\begin{eqnarray}z_{i,f}-z_{enc}\simeq -0.06z_{enc}+0.8\unicode[STIX]{x0394}z_{i}.\end{eqnarray}$$

The largest deviation from this linear behaviour occurs for weak wind conditions, $Fr_{0}\lesssim 10$ , where the turbulent and buoyancy Reynolds numbers in the entrainment zone are smallest in our DNS (see table 1). However, even in these cases, the linear behaviour is approached as the CBL – and accordingly the Reynolds number – grows, the deviation becoming less than 20 % for $z_{enc}/L_{0}\gtrsim 25$ . The data from the case $Fr_{0}=10$ and $Re_{0}=42$ further support this argument, since the deviation of these data from (4.8) at $z_{enc}/L_{0}=15$ decreases by $\simeq 33\,\%$ with respect to the case $Fr_{0}=10$ and $Re_{0}=25$ . To avoid this low-Reynolds-number effect from the weak shear cases, only the data from the cases $Fr_{0}>10$ are considered in the regression. Last, we also verified that the dependence of the regression coefficients on the threshold of $z_{enc}/L_{0}$ is small: the coefficients in $z_{i,f}\simeq 0.94z_{enc}+0.8\unicode[STIX]{x0394}z_{i}$ vary by $\simeq 2\,\%$ and $\simeq 5\,\%$ , respectively, as the threshold changes from $15$ to $20$ .

Figure 12.

Scaling of the flux-based and gradient-based CBL depths in the sheared CBL in terms of the encroachment length $z_{enc}$ , the EZ scale $\unicode[STIX]{x0394}z_{i}$ , and the Ozmidov length $(L_{Oz})_{z_{i,f}}$ . Light colours indicate low values of $z_{enc}/L_{0}$ , and dark colours indicate higher values of $z_{enc}/L_{0}$ .

We can easily find the limits of $\unicode[STIX]{x0394}z_{i}$ for weak wind conditions and strong wind conditions. For a vanishingly small wind, (4.8) has to recover (4.2), which implies that we can define

(4.9) $$\begin{eqnarray}(\unicode[STIX]{x0394}z_{i})_{c}\equiv 0.25z_{enc}\end{eqnarray}$$

as the asymptotic limit of $\unicode[STIX]{x0394}z_{i}$ when $Fr_{0}$ tends towards zero. This limit is indicated in figure 12(a) by the bold $\times$ symbol. We will refer to $(\unicode[STIX]{x0394}z_{i})_{c}$ as the convective limit of the EZ scale. To obtain the behaviour of $\unicode[STIX]{x0394}z_{i}$ for a strong wind, we use (4.5) to rewrite (4.6) as $\unicode[STIX]{x0394}z_{i}\simeq \sqrt{(Ri_{g})_{z_{i,f}}}\unicode[STIX]{x0394}u/N_{0}$ , where we have used the result $(\unicode[STIX]{x2202}_{z}\langle b\rangle )_{z_{i,f}}\simeq N_{0}^{2}$ shown in figure 11(b). Hence, as the wind strength increases and the gradient Richardson number decreases towards $1/3$ , $\unicode[STIX]{x0394}z_{i}$ asymptotically approaches

(4.10) $$\begin{eqnarray}(\unicode[STIX]{x0394}z_{i})_{s}\equiv \sqrt{1/3}\frac{\unicode[STIX]{x0394}u}{N_{0}}.\end{eqnarray}$$

We will refer to $(\unicode[STIX]{x0394}z_{i})_{s}$ as the shear limit of the EZ scale. When convection dominates in the entrainment zone, $(\unicode[STIX]{x0394}z_{i})_{s}$ is smaller than $(\unicode[STIX]{x0394}z_{i})_{c}$ , and the latter characterizes the lower EZ sublayer. As the wind intensity $U_{0}$ increases, $(\unicode[STIX]{x0394}z_{i})_{s}$ increases and eventually becomes comparable to $(\unicode[STIX]{x0394}z_{i})_{c}$ , at which point $(\unicode[STIX]{x0394}z_{i})_{s}$ starts to characterize the lower EZ sublayer. The weakly to strongly unstable conditions $-z_{enc}/L_{Ob}\gtrsim 4$ considered in this paper correspond to $(\unicode[STIX]{x0394}z_{i})_{s}/(\unicode[STIX]{x0394}z_{i})_{c}\lesssim 1.5$ . We will further explore in § 5 the capability of the ratio $(\unicode[STIX]{x0394}z_{i})_{s}/(\unicode[STIX]{x0394}z_{i})_{c}$ to characterize shear effects on entrainment-zone properties.

To characterize the upper EZ sublayer, we propose the following scaling law for the height of the maximum buoyancy gradient:

(4.11) $$\begin{eqnarray}z_{i,g}-z_{i,f}\simeq \unicode[STIX]{x1D6FE}_{s}\unicode[STIX]{x0394}z_{i}+\unicode[STIX]{x1D6FD}_{s}(L_{Oz})_{z_{i,f}}.\end{eqnarray}$$

This ansatz is motivated by (4.3), which indicates that, for shear-free conditions, the position of the upper EZ sublayer with respect to the lower EZ sublayer can be characterized by a linear combination of the scales characterizing the lower and upper sublayers. Figure 12(b) supports this ansatz, providing the coefficients $\unicode[STIX]{x1D6FE}_{s}\simeq 0.184$ and $\unicode[STIX]{x1D6FD}_{s}\simeq 1.78$ . The linear behaviour is also supported by the data corresponding to higher Reynolds-number simulations ( $Re_{0}=42$ ), although longer simulations would help to further validate (4.11). For vanishingly small $Fr_{0}$ , substituting $\unicode[STIX]{x0394}z_{i}$ by $(\unicode[STIX]{x0394}z_{i})_{c}$ in (4.8) and (4.11) recovers the shear-free result (4.3), which indicates that changes in the upper EZ sublayer due to wind shear are captured by the changes in $(L_{Oz})_{z_{i,f}}$ , the Ozmidov scale at $z_{i,f}$ . This further supports this length as a characteristic scale of the upper EZ sublayer. As the turbulence intensity in the lower EZ sublayer increases with respect to shear-free conditions, the lower EZ sublayer broadens and so does the upper EZ sublayer.

In summary, the entrainment zone in sheared CBLs can also be described as a composition of two sublayers, the lower EZ sublayer around the height of the minimum buoyancy flux, and the upper EZ sublayer around the height of the maximum buoyancy gradient. The difference from the shear-free case is that wind introduces a local scale $\unicode[STIX]{x0394}z_{i}$ in the characterization of the entrainment zone, in addition to the encroachment scale $z_{enc}$ and the Ozmidov scale $(L_{Oz})_{z_{i,f}}$ . The scaling laws for the reference heights are:

(4.12a ) $$\begin{eqnarray}\displaystyle & \displaystyle z_{i,f}\simeq 0.94z_{enc}+0.8\unicode[STIX]{x0394}z_{i}, & \displaystyle\end{eqnarray}$$

(4.12b ) $$\begin{eqnarray}\displaystyle & \displaystyle z_{i,s}\simeq 0.94z_{enc}+1.0\unicode[STIX]{x0394}z_{i}, & \displaystyle\end{eqnarray}$$

(4.12c ) $$\begin{eqnarray}\displaystyle & \displaystyle z_{i,g}\simeq 0.94z_{enc}+1.0\unicode[STIX]{x0394}z_{i}+1.78(L_{Oz})_{z_{i,f}}. & \displaystyle\end{eqnarray}$$

$\unicode[STIX]{x0394}z_{i}$

$(\unicode[STIX]{x0394}z_{i})_{c}$

$0.94z_{enc}$

$z_{i,0}$

$z_{i,s}$

$\unicode[STIX]{x0394}z_{i}$

$(L_{Oz})_{z_{i,f}}$

$z_{i,g}+1.78(L_{Oz})_{z_{i,f}}$

$z_{i,g}+1.78(L_{Oz})_{z_{i,f}}$

5.1 Scaling law for the EZ scale, $\unicode[STIX]{x0394}z_{i}$

To derive a scaling law for $\unicode[STIX]{x0394}z_{i}$ , we consider the integral analysis of the TKE balance equation discussed in § 2.4 but restricted to the entrainment zone:

(5.1) $$\begin{eqnarray}I_{t}^{EZ}=I_{T}^{EZ}+I_{P}^{EZ}+I_{bw}^{EZ}-I_{\unicode[STIX]{x1D700}}^{EZ}.\end{eqnarray}$$

Henceforth, the superscript $EZ$ stands for entrainment zone and indicates that the corresponding integral is calculated in the interval $z_{i,0}<z<z_{\infty }$ . To better quantify shear effects, we subtract the balance equation for the shear-free CBL from the balance equation for the sheared CBL, and we focus on the cases $Fr_{0}\gtrsim 15$ because wind-shear effects on entrainment-zone properties are small for smaller Froude numbers.

Figure 13.

Temporal evolution of the contributions from the accumulation term, $I_{t}^{EZ}$ , and the turbulent-transport term, $I_{T}^{EZ}=T_{z_{i,0}}-T_{z_{\infty }}$ , to the TKE budget equation (5.1). The subscript $c$ indicates the convective limit $Fr_{0}=0$ .

The shear enhancement of the accumulation term on the left-hand side of (5.1) is less than 10–20 % of the shear-production term for $z_{enc}/L_{0}\gtrsim 15$ (cf. figure 13 a) and hence negligible to leading order, which indicates a quasi-steady regime in the entrainment zone. The transport term can be written as

(5.2) $$\begin{eqnarray}I_{T}^{EZ}=T_{z_{i,0}}-T_{z_{\infty }},\end{eqnarray}$$

i.e. the difference between the transport of kinetic energy from the mixed layer into the entrainment zone and the transport of kinetic energy from the entrainment zone into the free atmosphere. As seen in figure 13(b), shear reduces the energy that is transported into the entrainment zone from the mixed layer and shear increases the energy that is radiated out into the free atmosphere by gravity waves, so that $I_{T}^{EZ}$ decreases with increasing shear. For weak shear conditions $Fr_{0}=5$ , the reduction of energy transported into the entrainment zone is larger than the enhancement of energy drained at the top (cf. figure 13 b), which suggests that shear sheltering (Hunt & Durbin Reference Hunt and Durbin1999) dominates over shear enhancement of gravity-wave radiation (Schröter Reference Schröter2018). This effect on the transport term for weak shear conditions, however, is not observed in the entrainment flux and viscous dissipation rate, which remain practically unchanged for $Fr_{0}\lesssim 10$ once the CBL is inside the quasi-steady regime (see also figures 5 a  and 7 a). We also see that the shear reduction of $I_{T}^{EZ}$ saturates and asymptotically approaches $\simeq 0.02w_{\ast }^{3}$ with increasing shear, where $w_{\ast }^{3}=B_{0}z_{enc}$ . This saturation is more clearly shown in figure 13(c), where we plot the flux difference across the entrainment zone as a function of the variable $\unicode[STIX]{x0394}u/[N_{0}(\unicode[STIX]{x0394}z_{i})_{c}]$ . (Using this independent variable is motivated by the results presented below.) Hence, as the shear production increases, the relative contribution of the turbulent transport in (5.1) decreases (cf. figure 13 d). For instance, the relative contribution is $\simeq 0.35I_{P}^{EZ}$ for $Fr_{0}=15$ and $\simeq 0.15I_{P}^{EZ}$ for $Fr_{0}=25$ . We also observe that data from cases with $Re_{0}=42$ coincide with data from cases with $Re_{0}=25$ within the statistical convergence reached in our simulations. Although the relative contribution of $I_{T}^{EZ}$ is arguably non-negligible for $Fr_{0}=15$ , the shear effect on entrainment-zone properties is still moderate for that Froude number, and therefore we neglect the turbulent transport terms in (5.1) as a first approximation; this approximation is validated below.

Shear effects on the viscous dissipation rate and the buoyancy flux are negligible for $Fr_{0}\lesssim 10$ once the CBL is inside the quasi-steady regime. For $Fr_{0}>10$ , figure 14(a) demonstrates that they are commensurate with each other,

(5.3) $$\begin{eqnarray}-[I_{bw}^{EZ}-(I_{bw}^{EZ})_{c}]\sim I_{\unicode[STIX]{x1D700}}^{EZ}-(I_{\unicode[STIX]{x1D700}}^{EZ})_{c},\end{eqnarray}$$

which indicates that energy destruction by viscous dissipation and by conversion to potential energy increase in a constant ratio independently of the shear strength in the equilibrium entrainment regime of the sheared CBL. The subscript $c$ indicates the convective limit $Fr_{0}=0$ . All these considerations, namely, using (5.3) and neglecting the accumulation term and the turbulent transport term in (5.1), yield the relationship

(5.4) $$\begin{eqnarray}(I_{bw}^{EZ})_{c}-I_{bw}^{EZ}\sim I_{P}^{EZ}.\end{eqnarray}$$

This relationship implies that the entrainment enhancement in sheared CBLs is due to the additional TKE generated by the wind shear in the entrainment zone.

Figure 14.

Scaling laws for the dominant terms in the TKE budget equation (5.1) as a function of the mean entrainment velocity, $w_{e}$ , the velocity jump across the entrainment zone, $\unicode[STIX]{x0394}u$ , the buoyancy stratification of the free atmosphere, $N_{0}^{2}$ , and the EZ scale, $\unicode[STIX]{x0394}z_{i}$ .

Here, we proceed further and use the structure analysis presented in § 4 to estimate the terms in (5.4) and thereby obtain a closed equation for the unknown $\unicode[STIX]{x0394}z_{i}$ . First, neglecting the thickness of the upper EZ sublayer, the integration intervals in (5.4) are well approximated by $\unicode[STIX]{x0394}z_{i}$ . Second, the velocity gradient can be scaled by its maximum value, $\unicode[STIX]{x0394}u/\unicode[STIX]{x0394}z_{i}$ (cf. (4.6)). Last, to estimate the fluxes of buoyancy and momentum, we use the entrainment-rate equations, which are obtained by integrating the evolution equations for the mean buoyancy and mean velocity from a height $z_{i,f}$ upwards (see appendix A). The entrainment-rate equations provide the scalings $-\langle b^{\prime }w^{\prime }\rangle _{z_{i,f}}\sim w_{e}\unicode[STIX]{x0394}b$ and $-\langle u^{\prime }w^{\prime }\rangle _{z_{i,f}}\sim w_{e}\unicode[STIX]{x0394}u$ . In these expressions,

(5.5) $$\begin{eqnarray}w_{e}\equiv \frac{\text{d}z_{i,f}}{\text{d}t}\end{eqnarray}$$

is the mean entrainment velocity, $\unicode[STIX]{x0394}b\equiv N_{0}^{2}\unicode[STIX]{x0394}z_{i}$ is a measure of the buoyancy increment across the entrainment zone, and the velocity jump $\unicode[STIX]{x0394}u$ is defined by (4.7). All these considerations indicate that the integrals on the left-hand side and right-hand side of (5.4) are scaled by $w_{e}\unicode[STIX]{x0394}b\unicode[STIX]{x0394}z_{i}$ and by $w_{e}(\unicode[STIX]{x0394}u)^{2}$ , respectively, which is confirmed by figure 14(b,c). Substituting these scaling laws into (5.4) yields

(5.6) $$\begin{eqnarray}w_{e}N_{0}^{2}(\unicode[STIX]{x0394}z_{i})^{2}-w_{e,c}N_{0}^{2}(\unicode[STIX]{x0394}z_{i})_{c}^{2}\simeq c_{1}w_{e}(\unicode[STIX]{x0394}u)^{2}.\end{eqnarray}$$

Figure 14(d) supports this ansatz and shows that $c_{1}\simeq 0.3$ . This coefficient can be interpreted as a modified Richardson number where the shear enhancement of the buoyancy flux is considered instead of the total buoyancy flux as in (4.1). This interpretation indicates that the values $(Ri_{f})_{z_{i,f}}\simeq 1$ observed when shear effects become relevant are significantly larger than the values 0.25–0.3 reported in marginally stable stratified shear flows because of the buoyancy flux caused by the turbulence in the CBL interior.

To use (5.6) to obtain a closed equation for the EZ scale, $\unicode[STIX]{x0394}z_{i}$ , we need to consider the mean entrainment velocity, $w_{e}$ . The shear enhancement of mean entrainment velocity, $w_{e}-w_{e,c}$ , can be split into two contributions by factorizing $z_{i,f}-(z_{i,f})_{c}$ as the product of $[z_{i,f}-(z_{i,f})_{c}]/z_{enc}$ and $z_{enc}$ , which yields

(5.7) $$\begin{eqnarray}w_{e}-w_{e,c}=\left[\frac{z_{i,f}-(z_{i,f})_{c}}{z_{enc}}+z_{enc}\frac{\text{d}}{\text{d}z_{enc}}\frac{z_{i,f}-(z_{i,f})_{c}}{z_{enc}}\right]w_{enc}.\end{eqnarray}$$

We have introduced the mean encroachment velocity $w_{enc}\equiv \text{d}_{t}z_{enc}$ , which can be written as $w_{enc}\simeq N_{0}L_{0}^{2}/z_{enc}$ by using (2.10). The first contribution is positive and represents a quasi-steady contribution to the shear enhancement of the entrainment velocity due to penetrative convection of a CBL that is deeper than in shear-free conditions. The second contribution is negative and represents the unsteady contribution due to the reduction of shear effects in time as the CBL grows and approaches the shear-free limit. As inferred from table 1, the ratio $[z_{i,f}-(z_{i,f})_{c}]/z_{enc}$ for $Fr_{0}=25$ changes less than 40 % when $z_{enc}$ changes by an order of one. Since $[z_{i,f}-(z_{i,f})_{c}]/z_{enc}$ is of the order of $0.15$ , neglecting the second term implies an error of $\simeq 5\,\%$ in the mean entrainment velocity $w_{e}$ , which suggests neglecting this unsteady contribution as a first approximation. With this approximation, the mean entrainment velocity can be written as

(5.8) $$\begin{eqnarray}w_{e}\simeq \frac{z_{i,f}}{z_{enc}}w_{enc}.\end{eqnarray}$$

Figure 15.

Verification with DNS data (coloured lines) of the scaling laws for the entrainment-zone properties derived in § 5 (dashed lines): (a) reference heights, (b,c,d) buoyancy-flux properties, (e) viscous dissipation rate, and (f) Ozmidov length.

Substituting (5.8) into (5.6), using the relationship $w_{enc}\simeq N_{0}L_{0}^{2}/z_{enc}$ , and using (4.12a ) to express $z_{i,f}$ in terms of $z_{enc}$ and $\unicode[STIX]{x0394}z_{i}$ , we can derive a cubic equation for $\unicode[STIX]{x0394}z_{i}/z_{enc}$ . This cubic equation, however, can be easily approximated by a simpler quadratic equation. To this end, we rewrite (5.6) as

(5.9) $$\begin{eqnarray}w_{e}[(\unicode[STIX]{x0394}z_{i})^{2}-(\unicode[STIX]{x0394}z_{i})_{c}^{2}]+(w_{e}-w_{e,c})(\unicode[STIX]{x0394}z_{i})_{c}^{2}\simeq 0.3w_{e}N_{0}^{-2}(\unicode[STIX]{x0394}u)^{2}.\end{eqnarray}$$

Approximating $w_{e}$ using (5.8), we can show that the ratio of the second to the first term satisfies

(5.10) $$\begin{eqnarray}\frac{(w_{e}-w_{e,c})(\unicode[STIX]{x0394}z_{i})_{c}^{2}}{w_{e}[(\unicode[STIX]{x0394}z_{i})^{2}-(\unicode[STIX]{x0394}z_{i})_{c}^{2}]}\simeq \frac{0.8(\unicode[STIX]{x0394}z_{i})_{c}^{2}}{[\unicode[STIX]{x0394}z_{i}+(\unicode[STIX]{x0394}z_{i})_{c}](0.94z_{enc}+0.8\unicode[STIX]{x0394}z_{i})}\lesssim 0.09,\end{eqnarray}$$

where the upper bound is obtained by using the inequality $(\unicode[STIX]{x0394}z_{i})_{c}<\unicode[STIX]{x0394}z_{i}$ and the definition $(\unicode[STIX]{x0394}z_{i})_{c}\equiv 0.25z_{enc}$ . This estimate is confirmed by the data, which show that the ratio of the second to the first term in (5.9) is less than 0.04 (not shown). Hence, we can neglect the second term in (5.9), which leads to

(5.11) $$\begin{eqnarray}\frac{\unicode[STIX]{x0394}z_{i}}{(\unicode[STIX]{x0394}z_{i})_{c}}=\left[1+0.3\left(\frac{\unicode[STIX]{x0394}u}{N_{0}(\unicode[STIX]{x0394}z_{i})_{c}}\right)^{2}\right]^{1/2}\end{eqnarray}$$

as an explicit expression for the EZ scale in terms of the controlling parameters and the velocity increment across the entrainment zone. The proposed scaling law for $\unicode[STIX]{x0394}z_{i}$ is supported in figure 15(a), where the reference heights $z_{i,f}$ and $z_{i,s}$ calculated by (4.12a ) and (4.12b ) using $\unicode[STIX]{x0394}z_{i}$ obtained from (5.11) agree with the DNS data. The small deviation between the scaling laws and the DNS data for $Fr_{0}=10$ and $15$ in figure 15(a) is due to the neglect of the turbulent flux of TKE in (5.1), but, as already indicated before, the shear effects in those cases are still relatively small. Comparing the data from cases $Re_{0}=25$ and $Re_{0}=42$ shows that the Reynolds-number dependence of these scaling laws is small, less than the achieved statistical convergence. Substituting the expression for $z_{i,f}$ , (4.12a ), into (5.8), we obtain

(5.12) $$\begin{eqnarray}\frac{w_{e}}{w_{e,c}}\simeq 0.82+0.18\frac{\unicode[STIX]{x0394}z_{i}}{(\unicode[STIX]{x0394}z_{i})_{c}}\end{eqnarray}$$

as an explicit expression for the mean entrainment velocity in the barotropic CBLs considered in this study. The convective limits are $w_{e,c}\simeq 1.14N_{0}L_{0}^{2}/z_{enc}$ , from (5.5) and (4.12a ), and $(\unicode[STIX]{x0394}z_{i})_{c}\equiv 0.25z_{enc}$ , from (4.9).

5.2 Scaling law for buoyancy-flux properties

Besides $z_{i,f}$ and $\unicode[STIX]{x0394}z_{i}$ , other properties that are relevant to characterize the entrainment zone are the ratio between the minimum turbulent buoyancy flux and the surface buoyancy flux, $-\langle b^{\prime }w^{\prime }\rangle _{z_{i,f}}/B_{0}$ , referred to as the entrainment-flux ratio (Pino et al. Reference Pino, Vilà-Guerau De Arellano and Duynkerke2003; Conzemius & Fedorovich Reference Conzemius and Fedorovich2006a ; Pino, Vilà-Guerau De Arellano & Kim Reference Pino, Vilà-Guerau De Arellano and Kim2006), and the square root of the ratio between the negative and positive areas of the turbulent buoyancy flux, $(-I_{bw}^{EZ}/I_{bw}^{ML})^{1/2}$ , where the superscript $ML$ stands for the mixed layer and indicates that the corresponding integral is calculated in the interval $0<z<z_{i,0}$ (Conzemius & Fedorovich Reference Conzemius and Fedorovich2006a ).

An estimate for $(-I_{bw}^{EZ}/I_{bw}^{ML})^{1/2}$ can be obtained as follows. From the relationship $-I_{bw}^{EZ}\sim w_{e}\unicode[STIX]{x0394}b\unicode[STIX]{x0394}z_{i}=w_{e}N_{0}^{2}\unicode[STIX]{x0394}z_{i}^{2}$ used before, estimating the corresponding coefficient of proportionality as 0.3 according to figure 14( $c$ ), and using the approximation $I_{bw}^{ML}\simeq 0.5B_{0}z_{enc}$ based on the linear variation of the turbulent buoyancy flux between the surface and $z_{i,0}$ (see figure 7 a), the area ratio can be expressed as

(5.13) $$\begin{eqnarray}\left[\frac{-I_{bw}^{EZ}}{I_{bw}^{ML}}\right]^{1/2}\simeq 0.21\frac{\unicode[STIX]{x0394}z_{i}}{(\unicode[STIX]{x0394}z_{i})_{c}}\left[0.82+0.18\frac{\unicode[STIX]{x0394}z_{i}}{(\unicode[STIX]{x0394}z_{i})_{c}}\right]^{1/2},\end{eqnarray}$$

where we have used (5.12) to express the result in terms of $\unicode[STIX]{x0394}z_{i}/(\unicode[STIX]{x0394}z_{i})_{c}$ . This scaling law is supported by the DNS data in figure 15(b). Consistent with previous work, we obtain a value $\simeq 0.2$ in the shear-free limit (Conzemius & Fedorovich Reference Conzemius and Fedorovich2006a ).

An estimate for $-\langle b^{\prime }w^{\prime }\rangle _{z_{i,f}}/B_{0}$ can be obtained in a similar way. From the scaling law $-\langle b^{\prime }w^{\prime }\rangle _{z_{i,f}}\sim w_{e}\unicode[STIX]{x0394}b=w_{e}N_{0}^{2}\unicode[STIX]{x0394}z_{i}$ employed before and using (5.12), we obtain

(5.14) $$\begin{eqnarray}\frac{\langle b^{\prime }w^{\prime }\rangle _{z_{i,f}}}{[\langle b^{\prime }w^{\prime }\rangle _{z_{i,f}}]_{c}}\simeq \frac{\unicode[STIX]{x0394}z_{i}}{(\unicode[STIX]{x0394}z_{i})_{c}}\frac{w_{e}}{w_{e,c}}\simeq \frac{\unicode[STIX]{x0394}z_{i}}{(\unicode[STIX]{x0394}z_{i})_{c}}\left[0.82+0.18\frac{\unicode[STIX]{x0394}z_{i}}{(\unicode[STIX]{x0394}z_{i})_{c}}\right].\end{eqnarray}$$

This scaling law is supported by the DNS data in figure 15(c). The deviation of $\simeq 20\,\%$ for strong wind conditions is a Reynolds-number effect. For the cases with $Re_{0}=25$ , the turbulent Reynolds number at $z=z_{i,f}$ , $(Re_{t})_{z_{i,f}}$ , is approximately four times larger for cases $Fr_{0}=20$ and $Fr_{0}=25$ than for case $Fr_{0}=0$ (1600 compared to 400, as seen in table 1). A similar variation in $Re_{t}$ is observed between cases $Re_{0}=25$ and $Re_{0}=117$ in shear-free conditions, and the entrainment-flux ratio in shear-free conditions, which is used to normalize the entrainment-flux ratio in sheared conditions, varies approximately 30 % over this interval of Reynolds number (see figure 16 a). Normalizing the minimum buoyancy flux for cases $Fr_{0}=20$ and $Fr_{0}=25$ with the approximation

(5.15) $$\begin{eqnarray}-\frac{[\langle b^{\prime }w^{\prime }\rangle _{z_{i,f}}]_{c}^{model}}{B_{0}}\simeq 0.12-0.45\left(\frac{z_{enc}}{L_{0}}\right)^{-1},\end{eqnarray}$$

which is derived in Garcia & Mellado (Reference Garcia and Mellado2014) from data at $Re_{t}\simeq 1600$ and hence turbulent Reynolds numbers that are comparable to the ones here in the strong shear conditions, (5.14) represents better the DNS data, as shown in figure 15(d).

Figure 16.

Temporal evolution of (a) the entrainment-flux ratio, $\langle b^{\prime }w^{\prime }\rangle _{z_{i,f}}/B_{0}$ , and (b) the normalized Ozmidov length particularized at the height of the minimum buoyancy flux, $(L_{Oz})_{z_{i,f}}/L_{0}$ , in the shear-free CBL. Symbols indicate the average within an interval $\unicode[STIX]{x0394}z_{enc}/L_{0}=2$ .

The scaling laws (5.13) and (5.14) do not feature a reduction of entrainment flux for weak shear conditions. The slight decrease observed in figure 15(c,d) for the case $Fr_{0}=5$ near $\unicode[STIX]{x0394}u/[N_{0}(\unicode[STIX]{x0394}z_{i})_{c}]=0.5$ is smaller than the statistical convergence of our data, as indicated in figure 15 by the shaded regions. Besides, those values correspond to an early stage of the quasi-steady regime, which is not observed in the case $Fr_{0}=10$ near $\unicode[STIX]{x0394}u/[N_{0}(\unicode[STIX]{x0394}z_{i})_{c}]=0.5$ , where the CBL is further into the quasi-steady regime and the local turbulent Reynolds number is six times larger. We recall that, for weak shear conditions, the analysis of the TKE budget equation presented in § 5.2 indicates that the shear production of TKE is mostly used to modify the transport of TKE in and out of the entrainment zone without significantly affecting the buoyancy flux and the dissipation rate, at least, to the accuracy achieved by our simulations.

5.3 Scaling law for the Ozmidov length

To reconstruct the complete entrainment-zone structure using (4.12) one needs a scaling law for the Ozmidov length $(L_{Oz})_{z_{i,f}}$ in addition to the scaling law (5.11) for the EZ scale $\unicode[STIX]{x0394}z_{i}$ . From the definition of the Ozmidov length (2.5), this implies obtaining a scaling law for the viscous dissipation rate at the height of minimum buoyancy flux. Such a scaling law can be obtained from the relationship (5.3), which states that changes in the dissipation rate relative to the shear-free limit are well scaled by the changes in the buoyancy flux, the constant of proportionality being $\simeq 0.3$ , as observed in figure 14(a). Hence, we can write

(5.16) $$\begin{eqnarray}\frac{I_{\unicode[STIX]{x1D700}}^{EZ}}{(I_{\unicode[STIX]{x1D700}}^{EZ})_{c}}\simeq 1+c_{2}\left[\frac{I_{bw}^{EZ}}{(I_{bw}^{EZ})_{c}}-1\right]\simeq 1+c_{2}\left[\frac{\unicode[STIX]{x0394}z_{i}^{2}}{(\unicode[STIX]{x0394}z_{i})_{c}^{2}}\frac{w_{e}}{w_{e,c}}-1\right],\end{eqnarray}$$

where the proportionality constant is $c_{2}\equiv -(I_{bw}^{EZ})_{c}/[0.3(I_{\unicode[STIX]{x1D700}}^{EZ})_{c}]$ and we have used the approximation $-I_{bw}^{EZ}\simeq 0.3w_{e}N_{0}^{2}\unicode[STIX]{x0394}z_{i}^{2}$ employed before to derive (5.13). The ratio of mean entrainment velocities in the equation above is provided by (5.12). To evaluate the proportionality constant $c_{2}$ , we know that $-(I_{bw}^{EZ})_{c}\simeq 0.022B_{0}z_{enc}$ by substituting $\unicode[STIX]{x0394}z_{i}=(\unicode[STIX]{x0394}z_{i})_{c}$ into (5.13), and we know that $(I_{\unicode[STIX]{x1D700}}^{EZ})_{c}\simeq (I_{T}^{EZ}+I_{bw}^{EZ})_{c}$ from the TKE budget equation for shear-free conditions, which yields $(I_{\unicode[STIX]{x1D700}}^{EZ})_{c}\simeq 0.048B_{0}z_{enc}$ when we use the estimate $(I_{T}^{EZ})_{c}\simeq 0.07B_{0}z_{enc}$ from figure 13( $c$ ). The value that we obtain is $c_{2}\simeq 1.53$ and the resulting scaling law (5.16) is validated with the DNS data in figure 15(e).

To find the scaling law for the Ozmidov length at $z_{i,f}$ , we define a characteristic scale for the dissipation rate in the entrainment zone as $I_{\unicode[STIX]{x1D700}}^{EZ}/\unicode[STIX]{x0394}z_{i}$ . From definition (2.5), we obtain the following ratio of the Ozmidov length between sheared conditions and shear-free conditions:

(5.17) $$\begin{eqnarray}\frac{(L_{Oz})_{z_{i,f}}}{[(L_{Oz})_{z_{i,f}}]_{c}}\simeq \left[\frac{(\unicode[STIX]{x0394}z_{i})_{c}}{\unicode[STIX]{x0394}z_{i}}\frac{I_{\unicode[STIX]{x1D700}}^{EZ}}{(I_{\unicode[STIX]{x1D700}}^{EZ})_{c}}\right]^{1/2}\simeq \left\{\frac{(\unicode[STIX]{x0394}z_{i})_{c}}{\unicode[STIX]{x0394}z_{i}}\left[1.53\frac{\unicode[STIX]{x0394}z_{i}^{2}}{(\unicode[STIX]{x0394}z_{i})_{c}^{2}}\frac{w_{e}}{w_{e,c}}-0.53\right]\right\}^{1/2},\end{eqnarray}$$

where the ratio of mean entrainment velocities is given by (5.12) as a function $\unicode[STIX]{x0394}z_{i}/(\unicode[STIX]{x0394}z_{i})_{c}$ . This scaling law is supported in figure 15(f). The deviation of $\simeq 20\,\%$ for strong wind conditions is a Reynolds-number effect, which, as explained in § 5.2, arises because the Ozmidov length in sheared conditions is normalized by the shear-free value, and the latter varies approximately 15 % within the interval of turbulent Reynolds numbers in the entrainment zone spanned between cases $Fr_{0}=0$ and $Fr_{0}=25$ (cf. figure 16 b). As a first approximation, one can consider

(5.18) $$\begin{eqnarray}\frac{[(L_{Oz})_{z_{i,f}}]_{c}}{L_{0}}\simeq \left[0.23{-}0.85\left(\frac{z_{enc}}{L_{0}}\right)^{-1}\right]^{1/2},\end{eqnarray}$$

which is obtained from definition (2.5), from (5.15) and from $(\unicode[STIX]{x2202}_{z}\langle b\rangle )_{z_{i,f}}\simeq 0.9N_{0}^{2}$ (see figure 11 b) and the observation that $(-\unicode[STIX]{x1D700}/\langle b^{\prime }w^{\prime }\rangle )_{z_{i,f}}\simeq 1.6$ according to figure 7(a). Normalizing the Ozmidov scale in sheared CBLs with the shear-free limit provided by (5.18) represents better the DNS data (not shown).