Stability of rubble mound breakwaters and shore revetments

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Extensive treatments on the stability of shore protection structures under the influence of waves and currents can be found in the Rock Manual [1], the Coastal Engineering Manual [2] and in textbooks such as the Introduction to bed, bank and shore protection (Schiereck, 1993) and Dikes and revetments (Pilarczyk, 1998).

This article provides a short introduction to the topic by summarising a few important notions, focusing on the example of rubble mound breakwaters and shore revetments.


Introduction

Shore protection structures are generally built to protect shorelines from ongoing erosion or to shelter areas from strong wave and current action. Shore protection structures can be divided into coastal (protection) structures and river (protection) structures. Here, the focus is on coastal structures. Coastal structures are e.g. breakwaters, dikes, revetments, groynes, seawalls/quay walls. They can either be monolithic (such as seawalls, caisson breakwaters or crest elements directly cast from concrete) or made of individual layers which interact with each other (e.g. armor layers of rock and/or artificial armor units, block revetments; underlayers made of rock, clay or sand and a structure core made of sand or rubble). A special category of coastal structures are gabions and geosystems (e.g. sand-filled geocontainers and geotubes); these structures are dealt with in the articles Artificial reefs and Sand-filled geosystems in coastal engineering. Coastal structures can influence the shoreline morphology in several ways; this influence is described e.g. in the articles Seawalls and revetments, Human causes of coastal erosion and Detached breakwaters.

Whereas rock and sand structures are flexible to some extent, monolithic structures are often rigid. In this article we focus on rubble mound breakwaters (RMB). The main advantages of these structures, compared to monolithic structures, are: (1) flexibility - the potential to accommodate (small) changes in seabed/beach level; (2) potential to dissipate wave energy, thus reducing wave loads on the structure, and also reducing the tendency for scour; (3) the (relatively) low costs of construction, maintenance and adaptation, especially for structures in limited water depth.


Design of shore protection structures

Shore protection structures can be built on the beach or offshore in the surf zone. In the first case the structure is essentially a revetment or dike protecting the backshore berm, dune foot or cliff base. In the second case the structure is a breakwater. Breakwaters can protect harbors from wave loading and wave penetration or, if built parallel to the shoreline, can aim to create sheltered depositional beaches. Offshore breakwaters can also serve to protect fairways and harbors from high waves.


Fig. 1. Left panel: Offshore rubble-mound breakwater. Right panel: Rock revetment protecting the backshore.


A typical design for a rubble mound breakwater is shown in Fig. 1. The basic design consists essentially of a sediment core, a geotextile, one or more granular underlayers, an armor layer of rock or concrete armor units and a toe structure. The functions of these components are:

  • The geotextile prevents erosion of the core and seabed by blocking the passage of sediment particles; however, it allows the passage of porewater. Care must be taken to ensure that the filter material is not damaged during installation. The geotextile must keep its filter function during the lifetime of the structure.
  • The granular underlayer protects the geotextile against puncturing by the overlying armor elements. It softens hydraulic pressure gradients, reduces lift forces on the armor elements and provides interlocking for the armor layer above. The recommended layer thickness is at least 60 cm and the grainsize 10-20 cm[2]. General guidelines for the stability and functionality of the underlayers are given in the Rock Manual[1]
  • The armor layer protects the underlayer/core against damage by wave action.
  • The toe prevents sliding of the armor elements along the slope of the structure, increases the geotechnical stability against macroscopic failure and prevents undermining of the structure due to scouring.

Rubble mound breakwaters can be subdivided into non-overtopped or marginally overtopped structures, low-crested (emergent and submerged), near-bed, reef-type breakwaters and reshaping (berm) breakwaters.

It is assumed that design conditions correspond to a situation with high waves and a strong wind- and wave-driven set-up of the mean water level. In this situation waves are breaking on the armor layer of the breakwater or the rubble-mound revetment protecting the backshore. Breaking waves may exceed the crest of the offshore breakwater, but this should not happen for the backshore protection. Hydrodynamic design conditions are discussed in the section #Determination of the design conditions.


Failure modes

Failure of a shore protection structure means:

damage that result in structure performance and functionality below the minimum anticipated design[2].

Several processes can cause failure of the shore protection structure; important processes are shortly described below.

Hydraulic instability of the armor layer

Armor layer instability due to wave loading is discussed in the section #Armor layer stability.

Scour (erosion) at the toe of the construction

Toe scour due to waves and currents is discussed in the section #Toe stability and bed/scour protection. Failure of the toe construction can cause sliding down of the armor layer.

Erosion of the rear side (lee side) of a rubble mound breakwater

The armor layer at the rear side must be designed to withstand erosion by overtopping waves (Fig. 2). The erosive power of overtopping can be reduced by the incorporation of a crown element[1], see Fig. 3. Wave overtopping is generally expressed as an average overtopping discharge per m width, [math]q \; [m^3/s/m][/math]. The overtopping discharge of a structure depends primarily on the significant wave height [math]H_s[/math] and on the relative crest height, [math]R_c/H_s[/math]. The freeboard [math]R_c[/math] is defined as the difference between the crest level of the structure and the still water level (SWL); it is positive for emerging crests and negative for submerged crests. Formulas for estimating the overtopping discharge [math]q[/math] for different types of structures are given in the Rock Manual[1], TAW (2002)[3] and Eurotop Manual (2018)[4], see Wave overtopping. The armor protection of the rear side of a breakwater should have similar size as the front side if the relative crest height [math]R_c/H_s \lt 0.3[/math]. If the relative crest height [math]R_c/H_s \gt 1[/math], hardly any wave overtopping will occur and the rear armor protection can be about three times smaller [1].

Erosion at the top of a berm protection revetment

The height of the rubble mound revetment should be determined such that wave run-up under design conditions does not produce significant erosion of the backshore, see Fig. 4. For wave run-up estimates on rubble mound breakwaters see: TAW (2002)[3], Eurotop (2018) [4] and Etemad-Shahidi et al. 2022[5].


Fig. 2. Erosion of the rear side of the breakwater due to overtopping waves.
Fig. 3. Breakwater with crown element.
Fig. 4. Overtopping of revetment by wave run-up and subsequent erosion.


Pore pressure and washout of particles from the core of the structure

Porewater flow due to a hydraulic pressure gradient inside the core can entrain fine sediment particles through the voids between the larger particles. The water table inside the core is generally higher than the mean water level (water inflow at the wave crest phase takes place over a larger cross-section than water outflow at the wave trough phase), implying on average higher outflow than inflow velocities. In the absence of an adequate filter, fine particles are washed out of the core. The voids inside the core gradually increase until the structure collapses. The presence of a geotextile or granular filter prevents the escape of sediment particles from the core. The openings of the filter should be small enough to prevent the passage of sediment particles. However, the openings must be large enough to drain excess porewater from the core.

The highest outward pressure along the breakwater slope (and highest pore water outflow) occurs around the time and location of maximum wave run-down. The outward directed pressure gradient is greatest in case of surging breakers which produce high wave run-up. This pressure gradient can exert a considerable lift force on the core material and armor layer. The highest shear stress levels also appear close to the time of maximum wave run-down level[6]. The submerged weight of the core material and the armor layer must be sufficient to offset these two forces.


Fig. 5. Principle of soil liquefaction. Left panel: Loosely packed skeleton of sediment particles in a water-saturated soil. Middle panel: When a heavy load is applied the pore pressure increases and the contacts between particles are broken; the free floating particles constitute a liquid soil. Right image: Drained compacted soil.

Soil liquefaction under the structure

A loosely packed saturated sandy seabed can liquify under heavy load. Depending on the initial density (water content) of the sand deposits, the clay content, water depth and wave characteristics, the presence of a structure may increase or decrease the liquefaction potential of the underlying sand deposits[7]. The risk of liquefaction is greatest with loosely packed well-sorted round sand particles, see Fig. 5. A seabed with a high content of clay particles can also liquify when loaded and subjected to strong pressure fluctuations (by wave action, seismic events)[8][9][10]. Surface waves generate cyclic shear strains in the soil. If the soil is loose (the skeleton of soil grains is compressible - quasi elastic), the cyclic shear strains will gradually rearrange and compact the soil grains at the expense of the pore volume of the soil. When the pores are largely filled with clay particles the permeability is low; porewater cannot flow out, leading to the buildup of excess pore pressure[11]. During this progressive buildup, the pore-water pressure may reach a level that exceeds the pressure of the overburden weight. The soil grains then become unbound and completely free, and the soil begins to act like a liquid. This process is called 'residual liquefaction', in contrast to the process of 'transient liquefaction' that can occur at the soil surface due to excess pore pressure under the trough of high surface waves. When the soil consolidates after liquefaction it is less susceptible to become liquefied again[8]. See also Wave-induced soil liquefaction.

Existing design methods based either on spectrum-based mean wave parameters or on significant wave parameters could grossly underestimate the liquefaction potential in silty sediment bed in field situations with random waves. Laboratory test show that infragravity waves have a strong impact, in spite of their relatively small amplitude[12].

Soil liquefaction destabilizes the seabed causing the structure to collapse, see Fig. 6. The susceptibility of a soil to liquefaction can be checked through Standard Penetration Tests or Cone Penetration Tests. Liquefaction risks can e.g. be reduced by replacing soft soil (expensive) or by consolidation measures. Soil consolidation can be done for example by vibro compaction or by preloading the soft bed with coarse sediment[13]. Monitoring of the consolidation process should ensure that a stable situation is reached.

Slip surface failure within the core

Slip surface failure can occur within the core (Fig. 7) or within the sediment body behind the revetment (slope instability)[14]. Slip surface failures develop when the effective shear stress (transmitted by contacts between sediment particles) on a slip plane exceeds a critical limit. In saturated sediment bodies, this critical limit decreases with increasing porewater pressure. Pore pressure builds up when fluctuations in the external pressure (by wave action, seismicity) cannot be levelled fast enough by porewater flow[8]. This can happen when the permeability of the sediment body is low, due to a high fraction of fine sediments. The permeability can be increased by the installation of drains. Coarse sand, gravel or quarry run are recommended as core material for rubble mound breakwaters[1]. The permeability of the geotextile must also be enough to prevent the development of excess pore pressures. A safe assumption is that the permeability of the geotextile must be at least 10 times that of the permeability of the fill material it is filtering, see Sand-filled geosystems in coastal engineering.

Instability of the foreshore

Waves and currents may generate sediment mobility. Interactions with the structure (e.g. wave reflection, wave draw-down, generation of turbulence) may result in scour of the bed or beach materials directly in front of the toe of the structure, with the potential to cause undermining. This erosion of the foreshore can then lead to slope instability and structural failure.


Fig. 6. Collapse of the armor layer due to seabed liquefaction under the toe of the breakwater.
Fig. 7. Slip failure of the core of the breakwater that may occur if the core is water saturated, insufficiently drained and subjected to cyclic loading.


Armor layer stability

The stability of a coastal structure is typically assessed by using various stability criteria (based on the various failure mechanisms). Stability criteria exist for the hydraulic and geotechnical stability of the entire structure and for individual structure parts (e.g. armor, filter, core). Structural failure (of a part of the structure) occurs if the respective stability criteria are not met.

Non-overtopped or marginally overtopped structures

Here we consider non-overtopped breakwaters (crest freeboard [math]R_c [/math] greater than the maximum wave run-up) or marginally overtopped breakwaters ([math]R_c \gt 0[/math]). It is assumed that the armor layer has been put in place properly, i.e., well packed such that there are many contact points between the armor elements. The functionality of the structure will be maintained during its intended lifetime if the armor elements stay largely in place with only small adjustments of their positions. This should be the case even under the heaviest wave attack considered in the design. The most crucial design parameters are the slope of the structure and the weight of the elements. It is recommended to optimize the design by means of hydraulic model tests, in order to achieve the best functionality at the lowest costs. This is especially true for situations with a complex geometrical setting. In the following, examples of empirical rules are presented that allow a rough initial estimate of the design parameters.

The stability or the armor layer is related to the significant wave height of the incident waves [math]H_s[/math] at the toe of the structure under design conditions. It is common to define the stability number

[math]N=\Large\frac{H_s}{\Delta \, D_{n50}}\normalsize , \qquad (1)[/math]

where [math]D_{n50}[/math] is the average diameter [m] of the armor elements (the median nominal diameter, corresponding to the mass of particles for which 50% of the granular material is lighter) and [math]\Delta=(\rho_r/\rho_w)-1[/math] is the relative density of the armor elements ([math]\rho_r, \rho_w[/math] are the densities of the armor elements and seawater, respectively). For rock [math]\Delta \approx 1.65[/math] and for concrete [math]\Delta \approx 1.3-1.4[/math]. The critical maximum value of the stability number [math]N_s[/math] for which the armor layer is stable, [math]N \le N_s[/math], depends on several parameters:

  • The slope [math]\alpha[/math] of the structure. The slope angle should not exceed the friction angle of about 35 degrees, i.e. [math]\cot \alpha \ge 1.5[/math] except for breakwaters with concrete armor layers which allow a steeper slope (for instance, [math]\cot \alpha=1.33[/math]); in earthquake-prone areas the critical slope angle is smaller.
  • The type of filter/underlayer.
  • The type of the armor elements (see Fig. 8).
  • The gradation of the armor elements (thumb rule: the size of the 20% smallest elements should not be smaller than half the size of the 20% largest elements).
  • The packing/porosity of the structure; the corresponding permeability parameter [math]c_p[/math] is defined as [math]c_p=[1 + (D_{core}/D_{armor})^{0.3}][/math], where [math]D_{core}, D_{armor}[/math] are the average particle sizes of the core and the armor layer, respectively.
  • The acceptable damage [math]S_d[/math] during the lifetime of the structure, defined as [math]S_d=A_e/D_{n50}^2[/math], where [math]A_e[/math] is the cross-sectional area eroded by wave action. Damage is sometimes expressed as the damage number [math]N_{od}[/math], the number of displaced units within a strip of width [math]D_{n50}[/math] across the slope; the relation between [math]N_{od}[/math] and [math]S_d[/math] can be approximated by[2] [math]N_{od} \approx G(1-p)S_d[/math], where [math]G[/math] = gradation factor, depending on the armor layer gradation ([math]G \approx 1.4[/math] for stone armor) and [math]p \approx 0.5[/math]= armor layer porosity. There is no unique relationship between 'acceptable damage' and 'loss of intended performance and functionality'. It depends on the type and the purpose of the structure[15]. Start of damage is often associated with values of [math]S_d[/math] of about 2 and 'failure' with values of about 12[1]. However, for reshaping structures and for structures with a very gentle slope the values are much higher. The stability of the structure is most threatened when the filter layer underneath the armor layer becomes exposed. The erosion depth (i.e. the reduction in thickness of the armor layer due to displaced stones) is therefore a more pertinent stability criterion rather than the eroded area ([math]A_e[/math] or [math]S_d[/math]) or the number of displaced stones [math]N_{od}[/math] [16].
  • The number of waves [math]n[/math] corresponding to design conditions (related to storm duration; often a maximum number [math]n[/math]=7500 is assumed).
  • The wave period of the design waves. The considered wave period is [math] T_{m-1,0}[/math]= mean energy period (definition given in Statistical description of wave parameters).
  • The steepness of the design waves. The wave steepness [math]s[/math] is defined as [math]s=2 \pi H_s/(g T_{m-1,0}^2)[/math].
  • The mode of wave breaking. The mode of wave breaking depends on the surf similarity parameter [math]\xi=s^{-1/2} \tan \alpha[/math]. For [math]\xi \gt 1.8 [/math] waves are surging and for [math]\xi \lt 1.8[/math] waves are plunging.
  • The slope of the foreshore [math]m[/math] (slopes between 1/100 and 1/30).

Wave flume experiments by Yuksel et al. 2022[17] revealed that the stability number also depends on the density of the armor elements; the stability number increases when normal concrete cubes are replaced with high-density cubes. This implies that using high-density cubes in a breakwater design provides economic efficiency with a significant decrease of concrete volume compared to normal-density cubes.

Several empirical formulas have been established for [math]N_s=\large\frac{H_s}{\Delta \, D_{n50}}\normalsize [/math], generally based on experiments in hydraulic models (laboratory flumes). One of the most simple and often used formulas is from Hudson (1959)[18]. It was derived from experiments with non-breaking regular waves, the water depth at the toe of the structure being much larger than the significant wave height. When written in terms of [math]H_s[/math] and [math]D_{n50}[/math] it reads

[math]N_s = \large \frac{(K_D \cot \alpha)^{1/3}}{1.27}\normalsize , \qquad (2)[/math]

where [math]\cot \alpha[/math] is the inverse average slope (width/height) of the structure. The factor [math]K_D[/math], the stability coefficient, depends on all other parameters listed above. A value of [math]K_D = 2[/math] is recommended in case of breaking waves and [math]K_D = 4[/math] in case of non-breaking waves. The formula is valid for a fixed damage level, namely 0–5 per cent of the armor stones displaced in the region of primary wave attack. Combining (1) and (2) an estimate can be derived for the required minimum weight [math]W = g \rho_r D_{n50}^3[/math] of cubic armor elements according to the formula of Hudson.

Next to the Hudson formula many stability formulae have been derived over the years for various armor and structure types and hydraulic boundary conditions. These formulae also include other relevant parameters, such as e.g. the wave period (breaker parameter) and permeability. An overview of stability formulas can be found in the Rock Manual[1] or the Coastal Engineering Manual[2]. Based on all available data Etemad-Shahidi et al. (2020) [19] derived a new optimal expression that takes into account the different parameters defined above:

[math]N_s = b \, c_p^{0.6} \, (\cot \alpha)^a \, s^{a/2} \, n^{-1/10} \, S_d^{1/6} \, (1-3m) , \qquad (3)[/math]

where [math](b=3.9 , a =1/3)[/math] for surging waves and [math](b=4.5, a=7/12)[/math] for plunging waves. The factor [math](1-3m)[/math] should be included only if the depth [math]h[/math] at the toe of the structure is less than [math]3H_s [/math].

For a structure with inverse slope [math]\cot \alpha = 1.5[/math] built on a [math]m=1/50[/math] sloping foreshore, with stone size ratio [math]D_{core}/D_{armor}=0.2[/math], subjected to [math]n=1000[/math] surging waves of design height [math]H_s[/math] and steepness [math]s=0.035[/math], the stability number according to Eq. (3) is given by [math]N_s \approx 1.3 \, S_d^{1/6}[/math]. Accepting a damage level of [math]S_d=4[/math], the safe diameter of the armor rocks is [math]D_{n50} \equiv D_{armor} \approx 0.35 \, H_s[/math].

The formula (3) has been empirically established for frontal wave attack. Oblique waves (wave incidence angle [math]\beta[/math]) have a smaller impact on the stability of the armor layer than frontal waves. This can be accounted for by multiplying formula (3) with a reduction factor [math]\gamma_{\beta}[/math] [20]. From analysis of flume experiments Van Gent (2014[21]) derived the formula [math]\gamma_{\beta} = c_{\beta} + (1- c_{\beta}) \, \cos^2 \beta[/math]. The coefficient [math]c_{\beta} \approx 0.44 [/math] for long-crested waves (small directional wave spreading) and [math]c_{\beta} \approx 0.6 [/math] for short-crested waves (large directional wave spreading).

In the flume experiments from which formula (3) is derived, only the influence of waves was considered. In field situations, strong wave action is often accompanied by strong winds. Strong winds can negatively affect the stability of the armor layer by increasing the wave run-up and run-down on the slope of the structure[22].

Fig. 8. Examples of concrete armor units. Not shown here are recent designs such as the Accropode II/Ecopode, Xbloc, Cubipod.


For high wave loads, requiring very large rock sizes (typically >10 ton), special concrete armor elements have been designed that provide better stability than rock armor, see Fig. 8. Experimentally determined stability numbers for randomly placed interlocking armor elements are in the range [math]N_s = 2 - 3[/math]. Interlocking concrete armor elements are susceptible to breakage[2]. Breakage of armor elements compromises the stability of the armor layer.


The formula (3) has been derived for structures with slopes in the usual range [math]1.5 \lt \cot \alpha \lt 6[/math]. On mild slopes ([math]\cot \alpha \gt 6[/math]), displaced rocks more often remain present in the wave attack zone, which increases the strength. This leads to an overdesigned structure when existing formulae for steep rock-armored slopes are used. On mildly sloping structures, especially in cases where these structures have a shallow foreshore, spilling waves will more frequently occur than plunging waves. Compared to steeper sloping structures, mildly sloping structures therefore show a wider part of the armor layer being affected by erosion and accretion. Accretion occurs at lower levels on the slope (reaching lower levels than two significant wave heights below the still water level) than for steeper slopes. Also, stones move both up and down, and more often remain in the wave attack section after displacement. This means that the same damage area corresponds to a smaller erosion depth for mild sloping structures compared to steep sloping structures[16]. It also means that the erosion depth is less slope dependent than the damage area.

There are situations where natural foreshores are formed if the structure has a mild slope with low wave reflection characteristics. For example, the natural foreshores in front of dikes in the Eastern and Western Scheldt estuaries in the Netherlands have slopes of 1:25 or gentler[16].

Low-crested breakwaters

Low-crested structures are defined here as structures overtopped by waves with their crest level close to the still water level (SWL). These structures can be subdivided in:

  • emergent structures with crest level above SWL: [math]R_c\gt 0[/math];
  • submerged structures with crest level below SWL: [math]R_c\lt 0[/math].

A further distinction can be made between statically stable and dynamically stable low-crested structures, also called reef breakwaters (see below).

Low-crested breakwaters are specifically designed to mitigate the attack of incoming waves and thereby protect beaches against erosion. While these structures only partially reduce incoming waves, they offer several advantages over high-crested breakwaters. They do not obstruct the view of the sea and allow water circulation and flushing between the structure and the beach. The distance between crest level and sea level (the so-called freeboard [math]R_c[/math]) is an important design parameter for low-crested breakwaters, as it influences the stability of the structure. Low-crested breakwaters transmit part of the incident waves. The wave transmission coefficient [math]C_t[/math] (ratio of transmitted wave height and incident wave height [math]C_t=H_{s, t}/H_{s, i}[/math]) depends mainly on the ratio of freeboard and incident significant wave height, the relative freeboard [math]R_c/H_{s, i}[/math]. The relationship between the transmission coefficient and the relative freeboard according to experimental data is shown in the graph of Fig. 9. Further details are given in Wave transmission by low-crested breakwaters.

For low-crested emergent structures a part of the wave energy can pass over the breakwater, see Wave overtopping. Therefore, the size or mass of the material at the front slope of such a low-crested structure might be smaller than on a non-overtopped structure. In the case of non-overtopped structures, waves mainly affect the stability of the front slope, while in the case of overtopped structures the waves do not only affect the stability of the front slope, but also the stability of crest and rear slope. Therefore, the size of the armor stone for these segments is more critical for an overtopped structure than for a non-overtopped structure.

As a rule of thumb the following formula of Kramer and Burcharth (2003)[23] can be used to obtain a first estimate of the stone size, [math]D_{n50}[/math] (relative density [math]\Delta=1.6[/math]). This formula has been derived for emergent structures in depth-limited wave conditions ([math]H_s/h=0.6[/math]), i.e. with breaking waves on a mild-sloping foreshore ([math]m \le 0.01[/math]) [1]:

[math]D_{n50} \ge 0.3 h , \qquad (4)[/math]

where [math]H_s[/math] is the significant wave height at the toe of the structure and [math]h[/math] is the water depth at the toe of the structure. Note that other values for [math]H_s/h, m, \Delta[/math] might lead to very different values for the stone size required. More detailed formulas on emergent structures are given in the Rock Manual[1].

Submerged structures

Submerged structures have their crest below the still water level (Fig. 9), but the depth of submergence of these structures is such that wave breaking processes affect the stability. Submerged structures are overtopped by all waves during design conditions and the stability increases considerably if the depth of submergence increases.

The stability criterion for submerged breakwaters is less severe (larger [math]N_s[/math]) than for emergent breakwaters, as far as the front armor layer is concerned. Therefore, smaller armor elements can be applied, with significant cost savings. However, the crest and the rear side of submerged breakwaters are relatively more vulnerable [24]. Damage at the rear side of the breakwater strongly affects the integrity of the whole structure, see Fig. 2. The size of the armor elements at the front side, the crest and the rear side should be similar if the freeboard is small, [math]|R_c|\lt 0.3 H_s[/math] [25].

Reshaping structures (Berm and reef breakwaters)

The berm breakwater is distinct from the classical breakwater by the addition of several stone layers at the seaward face. A wide berm (order 10 [math]D_{n50}[/math]) with berm crest around or above the still water level (design water level) can be very effective to reduce the wave runup and overtopping and to reduce damage to the armor layer[26]. Since the level of berms can be increased relatively easily once sea water levels increase, adding and/or modifying a berm is a useful measure for climate adaptation. Berm breakwaters can be differentiated into three types: Non-reshaping statically stable, Reshaped statically stable and Dynamically stable (reshaping) berm breakwaters.

For a non-reshaping statically stable berm breakwater the stability conditions are similar to a conventional breakwater, as armor stones are not allowed to move (or not more than a little bit to maintain the shape). Adding a second berm with berm crest below still water level can efficiently reduce the damage level in non-reshaping and partly reshaping breakwaters by changing the breaker type from surging to plunging and consequently providing a more stable (hardly reshaping) structure with less possibility of stone movement and breakage[27].

A dynamically stable (reshaping) berm breakwater is a design that allows reshaping of the breakwater profile into a more stable profile, where the individual stones may still move up and down the slope. If properly designed, reshaping increases the stability of the breakwater without compromising its functionality. Reshaping means that a larger damage factor is acceptable in Eq. (3). For a fully reshaping design (Fig. 10) the damage factor [math]S_d[/math] can be as large as 20. This larger damage factor implies a larger stability number (a factor 2 is possible) and consequently less severe conditions on armor stone size and breakwater slope. The cost savings compared to the conventional design can amount to 40% [13]. Design methods for dynamically stable berm breakwaters are given by Hall and Kao (1991)[28], Tørum et al (2003)[29] and Sigurdarson and van der Meer (2013)[30]. A cost saving design is a reshaping berm breakwater with smaller (class II) armor rocks on the less exposed lower part of the berm compared to the larger (class I) armor rocks on the more severely exposed upper part of the berm. The height of the upper part of the berm and its elevation above the design still water level are crucial design parameters for the stability of these two-class armor berm breakwaters. Empirical design formulas are given by Al-Ogaili et al. (2024[31]).

Reef-type structures are a special type of low-crested structure that can be reshaped by wave attack. They are dynamically stable, made of homogeneous material (stones) without a filter layer or core. A reef breakwater may initially be an emerged structure and after reshaping become a submerged structure. The equilibrium crest height after reshaping and the corresponding wave transmission are the main design parameters. Design methods for different types of reshaping structures can be found in the Rock Manual[1].


Fig. 9. Submerged breakwater. The freeboard is negative. The graph shows the range of values for the wave transmission coefficient obtained from experiments [1].
Fig. 10. Fully reshaping berm breakwater. The armor stones are allowed to move under severe storm conditions, during which the shape is adjusted to ensure greater stability.


Dynamic cobble revetment

Some field and laboratory experiments have been carried out to investigate whether a sandy backshore can be protected with a dynamic cobble berm revetment in the high-water wave-runup zone (cobbles are stones with a diameter in the range 64-256 mm)[32]. Although individual cobbles move up and down with each wave run-up, the experiments showed that the overall structure of the cobble revetment is maintained and undergoes a gradual small upward shift[32]. Installing a cobble berm revetment can be seen as a form of soft coastal defense. The cobble revetment is not intended to provide full protection against extreme storm surges but helps to prevent coastal erosion. Some sand leaching may take place from behind the cobbles, but this sand loss is strongly reduced if the revetment consists of poorly sorted material (due to the formation of a fine-gravel filter layer at the sand-revetment interface)[33]. Berm revetments made of poorly sorted angular gravel also are more stable than revetments of well-sorted rounded cobbles, due to better interlocking properties. As the gravel becomes rounder and some gravel is lost over time, renourishment may be necessary. There is no need to carefully place the renourishment material. It appears sufficient to simply dump the material on the revetment front face where it will be rapidly reshaped by wave action[33]. A cobble berm protecting an artificial dune can be a cost-effective protection of exposed shorelines, the expense being a small fraction of what it would have cost to construct a revetment or seawall[34].


Toe stability and bed/scour protection

The toe is a crucial component of a structure: it supports the armor layer and it prevents undermining by wave- and current-induced erosion. Different toe designs are possible; here we focus on toe structures consisting of loose elements, see Fig. 1. In some designs the toe is protected by sheet piles; these constructions will not be considered here. The seabed near the toe is susceptible to erosion. Therefore, the toe is often located below the seabed at the expected scour depth (right panel Fig. 1). If the seabed is not erodible, or if scour protection measures are applied, the toe can be situated on the seabed (left panel Fig. 1).

The toe is typically placed on a geofilter that prevents washout of fine sediment from below the toe. The geofilter is often protected by an underlayer of medium-sized stones on which larger toe elements are placed. The stability of the toe elements is ruled by considerations similar as for the armor layer. If the armorstone in the toe has the same size as the armorstone of the cover layer of the sloping front face, the toe is likely to be stable. The stability number for the toe elements is larger (up to factor 2) than for the armor elements if (under design conditions) the height of the toe (relative to the seabed) is much lower than the water depth under design conditions [1]. In that case the toe elements can be smaller than the armor elements. This has several advantages: less scour around the toe, less risk of soil liquefaction and lower costs. Formulas for the stability parameter [math]N_s[/math] of the armor protection of toe structures have been reviewed by Etemad-Shahidi et al. (2021[35]). They propose the formula

[math]N_s=\Large\frac{H_s}{\Delta \, D_{n50}}\normalsize =1.2 + 11.2 \, (h_t/h)^{7/4} \, (B_t/H_s)^{-1/10} \, s^{1/6} \, N_{od}^{2/5} \, (1 - 3.7 \, m) , \qquad (5)[/math]

with the same parameter definitions as for Eq. (3). [math]B_t/H_S[/math] is the relative toe width (cross-sectional toe width divided by significant wave height), [math]h_t/h[/math] is the relative toe depth (water depth on top of the toe divided by water depth in front of the toe) and [math]N_{od}[/math] is the number of displaced/washed away armor stones within a strip of width [math]D_{n50}[/math] across the structure. [math]N_{od}=0.5[/math] means start of damage which is generally considered as acceptable, [math]N_{od}=2[/math] means acceptable damage with some flattening out of the toe, and [math]N_{od}=4[/math] corresponds to failure and complete flattening out of the toe. If the toe is high ([math]h_t/h[/math] small) the structure is similar to a breakwater with a berm.

The risk of soil liquefaction under the toe (Fig. 5) has to be investigated by laboratory tests [36]. Soil compaction, soil replacement and/or draining measures may be needed for soils with a high fraction of fine sediments.

Fig. 11. Beach scour in front of a revetment; Delta Flume test.

Structures that disturb the natural flow induce a modification of the seabed morphology. Erosion dominates in the vicinity of these structures as a consequence of increased local energy dissipation of waves and currents. Empirical formulas for scour under the toe and in front of the toe were established by Den Bieman et al. (2019)[37], based on physical model tests with an impermeable core; in these tests ongoing erosion was observed without convergence to an equilibrium scour depth. As a rule of thumb, the maximum scour depth [math]S_m[/math] at vertical structures can be as large as the significant wave height [math]H_s[/math] under design conditions (with breaking waves)[2]. Erosion is greatest near the toe of reflective vertical structures. The scour depth is smaller for structures with a more gentle slope and a greater porosity. The scour depth is a decreasing function of the ratio water depth / wavelength (shorter waves tend to break against the structure, causing stronger erosion). The scour hole is typically located with in a distance of a quarter wavelength from the toe and closer to the toe for gently sloping structures[1].

Beach lowering occurs in front of structures protecting the backshore when waves collapse on the structure under storm conditions[38], see Fig. 11. Natural recovery of the beach level can occur under calm conditions in case of sufficient sand supply. In other cases, the option of artificial nourishment can be considered, see the articles Shore nourishment and Beach nourishment.

Fig. 12. Principle of the falling apron.

Obliquely incident waves generate a longshore current (see Shallow-water wave theory) that can strongly enhance erosion at the toe of the structure. This is particularly relevant for offshore breakwaters, where it is necessary to protect the seabed in front of the toe. This can be done with a stone cover, provided the stone size has been adjusted to the Shields criterion for critical shear stress (see Sand transport). An alternative is the so-called 'falling apron', a row of wide-graded quarry stone stacked at the edge of the toe. When a scour hole develops, the pile of stones falls into the pit and covers the bottom so that it does not erode further, see Fig. 12.

Significant scour can occur at the extremities (roundheads) of offshore shore-parallel breakwaters, especially for long breakwaters (length >> distance to the shore) and submerged breakwaters; this scour is largely due to currents driven by wave set-up landward of the breakwater (similar to rip currents) and to wave breaking over the roundhead. Deep scour holes of several tens of meters can form at the extremities of shore-perpendicular breakwaters (jetties and groynes) due to the combined action of currents (especially tidal currents near inlets) and storm waves[39][40]. Hence, particular attention is needed for scour protection of the seabed at the extremities of breakwaters. The use of a flexible mattress for protecting the seabed can be considered in case of very strong scour.


Shore protection structures such as breakwaters always require maintenance, in particular the repair of scour protection layers. An important point of attention for the design is therefore to ensure that the structure is easily accessible for maintenance.


Determination of the design conditions

Design conditions are the most destructive hydrodynamic conditions that the structure can resist without failing. More severe conditions must have a low probability of occurrence during the design lifetime. The structure may suffer some damage during design conditions, but this damage should not compromise the intended functionality of the structure. Conditions that occur more frequently should not produce damage, or the damage must be so small that the total accumulated damage during the design life of the structure remains within acceptable limits.

The ideal situation for investigating the lifetime of a structure is the availability of: (1) a record of field observations covering all hydrodynamic conditions relevant to the design, with a record length much longer than the design lifetime, and, (2) a hydraulic or numerical model capable to simulate the impact of the observed hydrodynamic conditions on the design for the entire duration of the observation record. With these tools the design can be optimized without the need to specify particular design conditions. However, this ideal situation hardly occurs in practice. A possible solution consists in constructing a dataset as intended under (1) from historical meteorological records, using a numerical hydrodynamic model – see, for example Morim et al. 2022[41].

The modelling step (2) is generally very demanding in time and costs. In practice, structures are tested in hydraulic and/or numerical simulation models for a selected set of hydrodynamic design conditions such as the Serviceability Limit State (SLS) and Ultimate Limit State (ULS). The SLS describes the performance of the structure under normal conditions. The ULS represents extreme events with a low probability of occurrence during the design lifetime (based on acceptable risk agreed between contractor and client). The extreme hydrodynamic conditions are derived from a statistical analysis of available data. The final verification of the design is usually performed using a physical model. The most important design parameters are:

  • The incident significant wave height [math]H_s[/math] at the toe of the structure (the 2% highest wave height [math]H_{2\%}[/math] is sometimes preferred);
  • The wave period [math]T[/math];
  • The wave incidence direction;
  • The extreme water levels;
  • The storm duration.

For offshore breakwaters in deep water, the extreme significant wave height and storm duration are usually the most critical design parameters. If available historical records of these parameters are too short for extracting directly the design values, they can be obtained from extreme value analysis. For the significant wave height this can be done, for example, by fitting significant wave heights above a certain threshold level to a Weibull distribution. The scour depth at the toe of the structure depends in general mainly on wave height and wave direction; frequent periods of energetic waves can be more relevant than exceptional extreme conditions. For estimating the scour depth, knowledge from field observations is required of the correlation between wave height and wave direction during such periods.

For breakwaters and revetments in shallow water the wave height is limited by depth-induced breaking. Deep-water wave data therefore have to be transformed to shallow water conditions (as explained in Shallow-water wave theory and Statistical description of wave parameters). The extreme water level is another important design parameter for structures in shallow water and on the beach: it determines the water depth above the toe of the structure and it influences the height of the waves breaking on the structure, the wave run-up and possible overtopping of the revetment. Extreme water levels are related to storm events and therefore correlate with extreme wave heights, but they are also influenced by the astronomical tide that is hardly correlated with wave height. The most critical combination of (extreme) water level and (extreme) wave height that may occur can be found by modelling the local hydrodynamic conditions with input from historical meteorological records and by constructing in this way a dataset of sufficient length. Other methods determine the joint probability of extreme water levels, wave heights and wave periods through statistical methods using copula functions – see for example Radfar et al. 2021[42], Li et al. 2021[43] and Vanem 2016[44].


Related articles

Wave overtopping
Wave transmission by low-crested breakwaters
Artificial reefs
Sand-filled geosystems in coastal engineering
Seawalls and revetments
Human causes of coastal erosion
Detached breakwaters
Wave-induced soil liquefaction
Statistical description of wave parameters
Shallow-water wave theory
Extreme storms
Wave collision on a vertical wall


Further reading

Schiereck, G.J. 1993. Introduction to bed, bank, shore protection. TU Delft, Department Hydraulic Engineering.
Pilarczyk, K. (editor) 1998. Dikes and Revetments. A.A. Balkema (publisher)

References

  1. ↑ 1.00 1.01 1.02 1.03 1.04 1.05 1.06 1.07 1.08 1.09 1.10 1.11 1.12 1.13 CIRIA/CUR/CETMEF 2007. The Rock Manual. The use of rock in hydraulic engineering (2nd ed.). C683. London: CIRIA
  2. ↑ 2.0 2.1 2.2 2.3 2.4 2.5 2.6 USACE, 2012. Coastal engineering manual. Report No 110-2-1100. Washington DC: US Army Corps of Engineers https://www.publications.usace.army.mil/USACE-Publications/Engineer-Manuals/u43544q/636F617374616C20656E67696E656572696E67206D616E75616C/
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The main authors of this article are Job Dronkers, Guido Wolters and Marcel van Gent
Please note that others may also have edited the contents of this article.
Citation: Job Dronkers; Guido Wolters; Marcel van Gent ; (2024): Stability of rubble mound breakwaters and shore revetments. Available from http://www.coastalwiki.org/wiki/Stability_of_rubble_mound_breakwaters_and_shore_revetments [accessed on 24-12-2024]
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